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A COMPARATIVE STUDY OF FREEZE—THAW PROCESSES FOR CONDITIONINGWASTEWATER AND WATER TREATMENT SLUDGES
by
•
Patti Gremillion Trahern
Dissertation submitted to the Faculty of theVirginia Polytechnic Institute and State University
in partial fulfillment of the requirements for the degree of
DOCTOR OF PHILOSOPHY
in
Environmental Engineering and Environmental Sciences
APPROVED:
W. R. Knocke, Chairman
gg „z„„„; K. (Z _¥_/¢—§_«,__4/G. D. Boardman P. C. Hoehn
gg gg 1,- ägäél
N R .. P. Wightman F. Sebba
g March, 1989Blacksburg, Virginia
A COMPARATIVE STUDY OF FREEZE-THAN PROCESSES FOR CONDITIONING
NASTENATER AND NATER TREATMENT SLUDGES
byPatti G. Trahern
N. R. Knocke, Committee Chairman
The Charles Edward Via, Jr., Department of Civil Engineering
Environmental Engineering and Environmental Sciences
(ABSTRACT)
This research effort involved the application of indirect- and
direct-contact, freeze—thaw conditioning techniques for improving the
dewatering characteristics of both wastewater and water treatment
sludges. Sludges tested included waste activated sludge, primary
sewage sludge, waste activated/primary sewage sludge mixtures and
alum sludge. The direct-freeze methods examined were the use of a
secondary refrigerant (butane) evaporated in the sludge and the use
of gas hydrate or clathrate formation by addition of Freon 12 under
appropriate temperature and pressure conditions. Sludges were also
frozen solid using indirect freezing methods, thawed and tested for
comparative purposes. Particle size distribution and floc density
measurements were used to determine changes in particle characteris-n
tics; specific resistance values and dewatered dry solids concen-
tration were used to assess dewatering characteristics. Results of
direct- and indirect-contact, freeze—thaw conditioning were compared
to the effects of polymer conditioning. The results indicated that
direct-freeze methods do not appear technically or economically
competitive with currently accepted conditioning methods. The
superior results obtained with the indirect-contact, freeze-thaw
process when compared to the direct—contact processes suggested that
the extent and rate of freezing may greatly influence the particle
characteristics of the conditioned sludge, and thus its dewatering
characteristics.
ACKNOWLEDGEMENTS
TABLE 0F CDNTENTS
PageI. INTRODUCTIDN 1
II. LITERATURE REVIEW 4Evaluating Conditioning Effectiveness 4Specific Resistance 4
Compressibility 11Blinding 12The Relationship of Particle
Characteristics to Specific Resistance 15
Freeze-Thaw Processes 18Natural Freeze-Thaw Conditioning 19Indirect—Contact, Freeze-Thaw Conditioning 21Direct-Contact, Freeze-Thaw Conditioning 22
Impact of Process and Handling variables onEffectiveness of Freeze-Thaw Conditioning 57
Rate and Extent of Freezing 57Chemical Addition 59Storage 60Thickening 61Handling and Mixing 62
Mechanisms of Freeze-Thaw Conditioning 63
Solids Migration and Compression 63Particle Dehydration and Cell Rupture 65Role in Direct-Contact Processes 66
III. METHODS AND MATERIALS 68 ßSludge Sources 68
Waste Activated Sludges 68Primary Sewage Sludge 69Alum Water Treatment Sludges 70
v
TABLE OF CONTENTS(continued)l
Page
Conditioning Methods 71
Direct-Contact, Freeze-Thaw Conditioningwith Butane 71
Direct-Contact, Freeze-Thaw Conditioningwith Dichlorodifluoromethane (Freon 12) 73
Indirect-Contact, Freeze-Thaw Conditioning 76Polymer Conditioning 76
Experimental Apparatus 79
Reactors 79Heat Exchange Systems 83Refrigerant Feed Systems 85Conditioning Agent Removal 89
Analytical Methods 90
Particle Size Distribution 90Specific Resistance, Initial and
Vacuum-filtered Solids Concentration,and Blinding Coefficient 93
Centrifuged Solids Concentration 93Floc Density 94Total Organic Carbon 94Sludge pH 95
IV. RESULTS 96
Stroubles Creek waste Activated Sludge 96
Polymer Conditioning 96Indirect-Contact, Freeze-Thaw Conditioning 101Direct—Contact, Freeze-Thaw Conditioning
with Butane 106Direct-Contact, Freeze-Thaw Conditioning
with Freon 12 115
vi
TABLE 0F CONTENTS Qcontinued)
Page
Stroubles Creek Primary Sewage Sludge 125
Polymer Conditioning 125Indirect-Contact, Freeze—Thaw Conditioning 130Direct-Contact, Freeze—Thaw Conditioning
with Butane 136Direct-Contact, Freeze-Thaw Conditioning
with Freon 12 140
Stroubles Creek Primary Sewage Sludge/wasteActivated Sludge Mixture 144
Polymer Conditioning 144Indirect-Contact, Freeze-Thaw Conditioning 148Direct-Contact, Freeze-Thaw Conditioning
with Freon 12 151
RAAP Alum Sludge 157
Effects of Dilution 157Polymer Conditioning 158Indirect-Contact, Freeze—Thaw Conditioning 166Direct-Contact, Freeze-Thaw Conditioning
with Butane 174Direct-Contact, Freeze-Thaw Conditioning
with Freon 12 183
V. DISCUSSION 196
Proposed Mechanism for Freeze-Thaw Conditioning 197
Disruption of Sludge Structure 197Formation of New Floc Structure 204
Evaluation of Direct-Contact Freeze-ThawConditioning
210Particleand Chemical Characteristics 210Dewatering Characteristics 215
vii
TABLE OF CONTENTS (continued)
Page
Comparison with Other Studies and ProcessViabiTity 219
Butane Conditioning 219Freon Conditioning 220Process Viabi1ity 221
VI. CONCLUSIONS 223
VII. LITERATURE CITED 226
viii
LIST 0F TABLES
TableNo. Title Page
1 Selected Results of Direct-Contact, Freeze-Thaw Conditioning of waste ActivatedSludges with Butane 37
2 Decomposition Temperature and Pressureof Hydrating Agents 51
3 Selected Results of Direct-Contact, Freeze-Thaw Conditioning of WastewaterSludges with Freon 56
4 Experimental Matrix 72
5 Butane Vapor Saturation Data 74
6 Freon 12 Vapor Saturation and Gas HydrateEquilibrium Data 77
7 Experimental Analyses and Determinations 91
8 Results of Analyses, Polymer-Conditionedwaste Activated Sludge 98
9 Results of Analyses, Indirect-Contact,Freeze-Thaw-Conditioned wasteActivated Sludge 102
10 Results of Analyses, Butane-Conditionedwaste Activated Sludge 108
11 Results of Analyses, Freon-Conditionedwaste Activated Sludge (Batch 117Experiments)
12 Results of Analyses, Freon-Conditionedwaste Activated Sludge (ContinuousExperiments) 118
13 Results of Analyses, Polymer—ConditionedPrimary Sewage Sludge 126
ix
LIST OF TABLES (continued)
TableNo. Title Page
14 Results of Analyses, Indirect-Contact,Freeze—Thaw-Conditioned PrimarySewage Sludge 133
15 Results of Analyses, Butane—ConditionedPrimary Sewage Sludge 137
16 Results of Analyses, Freon-ConditionedPrimary Sewage Sludge (BatchExperiments) 142
17 Results of Analyses, Polymer-ConditionedPrimary Sewage/waste Activated SludgeMixtures 146
18 Results of Analyses, Indirect-Contact,Freeze-Thaw-Conditioned PrimarySewage/waste Activated Sludge Mixtures 148
19 Results of Analyses, Freon-ConditionedPrimary Sewage/waste Activated SludgeMixtures (Batch Experiments) 153
20 Results of Analyses, Undiluted, Polymer-Conditioned Alum Sludge 160
21 Results of Analyses, Diluted, Polymer-Conditioned Alum Sludge 164
22 Results of Analyses, Undiluted, Indirect-Contact, Freeze-Thaw-Conditioned AlumSludge 167
23 Results of Analyses, Diluted, Indirect-Contact Freeze-Thaw-Conditioned AlumSludge 172
‘
24 Results of Analyses, Undiluted, Butane-‘
Conditioned Alum Sludge 175
x
LIST 0F TABLES (continued)E
TableNo. Title Page
25 Results of Analyses, Diluted, Butane-Conditioned Alum Sludge 184
26 Results of Analyses, Undiluted, Freon-Conditioned, Alum Sludge (BatchExperiments) 185
27 Results of Analyses, Diluted, Freon-Conditioned, Alum Sludge, (ContinuousExperiments) 186
28 Results of Analyses, Diluted, Freon-Conditioned Alum Sludge (BatchExperiments) 189
29 Results of Analyses, Diluted, Freon-Conditioned Alum Sludge (ContinuousExperiments) 190
30 Effect of Indirect—Contact, Freeze-Thaw Conditioning on FlocCharacteristics 198
31 Effect of Indirect-Contact, Freeze-Thaw Conditioning on ChemicalCharacteristics 202
32 Effect of Indirect-Contact, Freeze-Thaw Conditioning on ParticleCharacteristics 206
33 Effect of Indirect—Contact, Freeze-Thaw Conditioning on DewateringCharacteristics 208
34 Effect of Direct—Contact, Freeze-Thaw Conditioning on ParticleCharacteristics 211
35 Effect of Freon Conditioning onFloc Characteristics 213
xi
LIST OF TABLES (continued)
TableNo. Title Page
36 Effect of Direct-Contact, Freeze-Thaw Conditioning on DewateringCharacteristics 216
xii
LIST 0F FIGURES
FigureRg; Title Page
1 Characteristic Dewatering Response forUnblinded and Blinded Sludge Samples 10
2 Typical Process Flow Schematic forSecondary Refrigerant Desalination 28
3 Types I and II Gas Hydrate Structures 42
4 Generalized Gas Hydrate Phase Diagram 45
5 Butane Vapor Saturation Curve 75
6 Freon 12 Vapor Saturation and GasHydrate Equilibrium Curves 78
7 Schematic of Direct—Contact Freeze-Thaw Conditioning Apparatus 80
8 Particle Size Distributions, Polymer-Conditioned waste Activated Sludge 99
9 Particle Size Distributions, Indirect-Contact, Freeze-Thaw-Conditionedwaste Activated Sludge 104
10 Particle Size Distributions, wasteActivated Sludge Conditioned with400 mL/L Butane 109
11 Specific Resistance vs. Butane Dose,Butane-Conditioned waste ActivatedSludge 112
12 Particle Size Distributions, Freon-Conditioned waste Activated Sludge(Batch Experiments) 119
13 Particle Size Distributions, Freon-Conditioned waste Activated Sludge(Continuous Experiments) 120
xiii
LIST 0F FIGURES (continued)
FigureHg; Tit1e Page
14 Specific Resistance vs. Freon Dose, Freon-Conditioned waste Activated Siudge 124
15 Particie Size Distributions, Po1ymer—Conditioned Primary Sewage Siudge 129
16 Specific Resistance vs. Po1ymer Dose,Po1ymer—Conditioned Primary SewageSiudge 131
17 Particie Size Distributions, Indirect-Contact, Freeze-Thaw-ConditionedPrimary Sewage Siudge 134
18 Particie Size Distributions, PrimarySewage S1udge Conditioned with800 m1/L Butane 139
19 Particie Size Distributions, Freon-Conditioned Primary Sewage Sludge(Batch Experiment) 143
20 Particie Size Distributions, Indirect-Contact, Freeze-Thaw ConditionedPrimary Sewage /waste Activated SiudgeMixture 150
21 Particie Size Distributions, Freon-Conditioned Primary Sewage/wasteActivated S1udge Mixture (BatchExperiment) 155
22 Partic1e Size Distributions, Undiiuted,Poiymer-Conditioned A1um S1udge 161
23 Partic1e Size Distributions, Diiuted,PoIymer—Conditioned A1um Siudge 165
24 Partic1e Size Distributions, Undiiuted,Indirect-Contact, Freeze-ThawConditioned A1um Siudge 169
xiv
LIST 0F FIGURES (continued)
Figuregg; Tit1e Page
25 ParticIe Size Distributions, DiIuted,Indirect-Contact, Freeze-ThawConditioned Alum Sludge 173
26 ParticIe Size Distributions, UndilutedAlum Sludge Conditioned with 400 mI/LButane 178
27 Particle Size Distributions, UndiIutedATum Sludge Conditioned with600 mL/L Butane 179
28 Specific Resistance vs. Butane Dose,UndiIuted, Butane-ConditionedA1um Siudge 181
29 ParticIe Size Distributions, Diluted,Freon-Conditioned AIum Siudge (BatchExperiments) 191
30 Particle Size Distributions, Diluted,Freon-Conditioned AIum Sludge (ContinuousExperiments) 192
31 Specific Resistance vs. Freon Dose,DiIuted, Freon-Conditioned A1um Sludge 194
xv
LIST OF APPENDICES
Appendixgg; Title Page
A Oesignations for Halogenated Halocarbons 233
xvi
I. INTRODUCTION
Sludge production is an inevitable result of many wastewater and
certain water treatment processes. These solids must be stabilized,
sometimes thickened and conditioned, and then dewatered before
ultimate disposal. For most sludge generators, disposal methods are
limited to landfilling, incineration, and other processes, the costs
of which depend upon the volume of the sludge to be disposed. The
drier the sludge, the more efficient and less expensive the process
usually is.
Sludge conditioning is selectively undertaken for one of two
purposes: (1) to improve the dewatering rate of a sludge (i.e., to
decrease the amount of time required to remove a given amount of
water from the sludge); and (2) to improve the extent of dewatering
or thickening (i.e., to increase the amount of water removed from the
sludge.) In addition, conditioning is frequently necessary to obtain
an easily handled product.
Conditioning can decrease the resistance of sludge to dewatering
to one percent or less of the original resistance of the
unconditioned sludge. It typically reduces moisture content from
about 95 to 98 percent to about 60 ix: 75 percent for the final
dewatered productl._
Freeze-thaw conditioning occurs when sludge is allowed to come
into contact with air, water vapor, a secondary refrigerant, or other
1
freezing agent under temperature and pressure conditions conducive to
freezing. Freezing may occur naturally (for example, when lagooned
water sludges freeze during extended periods of cold weather) or may
be artifically induced by indirect or direct contact between sludge
and a refrigerant.
Freeze-thaw conditioning can produce an extremely dry, grainy,
odorless product composed of up to 60 to 70 percent solidsz. Such
conditioning often increases the solids handling capacity (e.g.,
filter yield) of mechanical dewatering equipment. In fact, certain
sludges drain so easily following freeze-thaw conditioning that there
is no need for thickehing or filtration after conditioning if
sufficient land is available for gravity dewateringß. Freeze-thaw
processing has been used to condition a wide variety of sludges,
including water treatment sludges as well as domestic and industrial
wastewater sludges.
With the exception of natural freezing, processes used to freeze
sludge are often technically complex, expensive, and energy
intensive. Natural freezing requires large areas of land for proper
lagooning and storage. Nevertheless, these disadvantages may be
offset by the unusually high solids concentrations made possible by
freeze-thaw conditioning, and the tractable nature of the product
sludge.
The results obtained from freeze-thaw conditioning must be
evaluated against the standards set by chemical conditioning. The
addition of inorganic metal salts (e.g., ferric chloride, aluminum
2
hydroxide, ferrous sulfate, and lime) as conditioning agents has a
long history of successful employment in water and wastewater
treatment practice. Likewise, polymer conditioning has become
increasingly popular.
The purposes of this investigation were:
1. to develop methods for direct-contact, freeze-thaw
conditioning processes;
2. to use these methods to condition a variety of sludges;
3. to compare the results of direct-contact, freeze-thaw
conditioning to indirect-contact, freeze-thaw conditioning
and polymer conditioning.
4. to develop a model of the freeze-thaw process.
3
II. LITERATURE REVIEW
A review of the literature was conducted to develop a technical
and historical context for the current investigation. This review
addresses the following specific goals:
— to evaluate methods of evaluating conditioning
effectiveness, i.e., improvements in the rate and
extent of dewatering of conditioned sludges, and to
determine which methods were appropriate to theE current investigation;
- to research process descriptions and histories for
freeze-thaw processes as background for selection of
freeze-thaw methods and agents;
- to assess the impact of process and handling variables
on the effectiveness of freeze-thaw conditioning in
past studies as background for development of
freeze-thaw techniques; and
- to present proposed mechanisms of freeze-thaw
conditioning. r
· 4
EVALUATING CONDITIONING EFFECTIVENESS
The parameters of interest in evaluating the effectiveness of
conditioning methods and agents are the rate and the extent of sludge
dewatering. For most sludges, these dewatering characteristics are
dependent upon factors such as particle size distribution, floc water
content, and other properties. Common measures of dewatering
characteristics--—specific resistance and compressibility---are
calculated using equations predicated on these variables. These
parameters and their derivations are introduced in this section. The
physical phenomenon of blinding and its matnematical relationship to
specific resistance are also presented. Finally, the relationships
of particle size and other sludge particle characteristics to
specific resistance are reviewed.
Specific Resistance
The specific resistance of a sludge is a measure of the relative
ease (or difficulty) with which filtrate flows through the cake
formed as sludge drains under an applied vacuum. The lower the
specific resistance, the easier the sludge is to dewater. This
parameter is defined as the resistance per unit weight of dry cake
solids per unit volume of filtrate collected and is expressed in
units of length per mass (m/kg).
Specific resistance is calculated from the data obtained from a
laboratory procedure known as the Buchner funnel test. The test is
conducted using an apparatus consisting of a Buchner funnel secured
5
atop a graduated cylinder. The desired vacuum (pressure
differential) is applied and the amount of filtrate removed from the
sample over the period of filtration is recorded at intervals. The
time required for the filter cake to crack is noted, and the final
cake solids concentration determined on a sample of the filter cake
as well.
Although the Buchner funnel procedure bears a closer resemblance
to vacuum filtration than to other methods of dewatering, its
accuracy in predicting vacuum filter _yields is arguable4'6. Its
usefulness in differentiating among conditioning methods and doses
for a given sludge is, however, generally accepted.
For a given sludge with a specific initial solids
concentration, the time required to obtain a specified volume of
filtrate, or the time required for the filter cake to crack, gives a
rough estimate of dewatering rate. The usefulness of this estimate
is limited, however, since these data do not predict sludge behavior
over a range of solids concentrations. In addition, fibrous or poorly
dewatering sludges may produce a cracked cake only after an
inordinately long filtration period, or not at all.
A more useful calculation obtained from the data collected in
the Buchner funnel test yields specific resistance. The concept and
derivation of this parameter is based upon equations fundamental to
filtration theory. The basic equation is Darcy's law, which statesP
dV = (P) (AK) [1]df TT
6
where
dV/dt = rate of flow (volume of filtrate
collected per unit time);
P = pressure difference
A = area
p = viscosity
K = permeability
L = thickness.
Stated simply, the change in filtrate volume with time, dV/dt,
is proportional to three variables: (1) the area of filtration, A,
(2) the pressure applied across the material filtered (medium and
sludge cake), P, and (3) the permeability of the medium and the cake,
K. The change is inversely proportional to the viscosity, u, and to
the thickness of the cake, L.
The resistance R is defined as the inverse of the permeability.
Substitution of R for 1/K in Equation 1 yields:
EUR5. [21dt uLR
where R is the combined resistance offered by the filter paper (Rm)
and the cake resistance (RC). These two resistances are sometimes
considered separately 6’7. It is argued that the initial resistance
offered by the filter before the cake begins to form is significant
when compared to the resistance offered by the sludge. The two
7
resistances can be considered, however, a single factor if filter
media resistance is always negligible when compared to cake
resistance5. Significant filter resistance is usually caused by
filter clogging by sludge particles, in which case the resulting
increase in resistance is due to the sludge itself.
This disagreement has led to differences in the method used to
acquire the data used to determine specific resistance. Gale7
recommended ignoring the first filtrate to pass through the filter
and noting volume only when the filter resistance relative to the
cake resistance is negligible. Notebaert5 recommended recording
filtrate volume as soon as the first filtrate is released. In this
study the protocol suggested by Notebaert's argument was used, and
the corresponding derivation is presented here.
The specific resistance r is defined as the resistance per unit
weight of dry cake solids. It can be expressed as:
r=By [3]w
where
R = combined resistance per unit volume of filtrate
v = volume of cake deposited per unit filtrate volume
w = filter cake deposited per unit volume of filtrate
The solids loading term vv may be determined from a rnaterial
8
balance:
w = Ckco1
[4]
where CO and Ck are the initial and final cake solids concentrations,respectively.
In order to introduce the specific resistance r into Equation I,
vV is substituted for AL:
area?. psidt p vVR
Substituting rw for Rv, Equation 3 becomes:
_ 2Q!·E./L I6]dt u Vrw
Equation 6 can then be rearranged to:
dt = (uVrw)dV [7](PA)
Assuming pressure changes during the test are negligible, Equation 7
can be integrated to obtain:
_ 2t — prwV [8]' 2PA2
Equation 8 can be rearranged in the form y = bx, as shown in Figure
Ia:
E = V BKHZ [9]V 2PA
‘ 9
II.I / _
//x
>\ .I-
slopa = b = ufw/2PA2
V18. SCHEHRTIC DIHGRHH OF TYPICRL BUCHNER FUNNEL F1LTR8•
TION O8T8 FOR SLLIISE EXHIBITING NO BLINOIPG PI·£NOHEN8
‘·* RT /LIJ /(_) /Z /
//
LD / /Rc
1-1
Ü ///uf /1_1 /’ Ru11.1 /CL(D
VII. SCHEHRTIC O186R8H OF r FOR 8 HEOIUHSLIMIO SLUOGE
DJLJZGIl•U')•—•
13 “}/Q , / Rc ·.1.1 ’Ü ’ : ..(D
V1C. SCHEHBTIC 0186888 OF r FOR 8 CRKE-BLINOED SLUDSE
FIGURE 1. CHFIRHCTERISTIC OEURTERING RESPONSE FORUNBL INDED RND BLINDED SLUDGE SRMPLE5.
10
The slope of the line t/V vs V is:
b = [10]
The specific resistance is then defined:
r = 2PA2b [11]pw
This resistance is an average value, being predicated upon an
average cake solids content, a constant pressure drop across the
cake, and the assumption that any filtrate squeezed from the cake
itself is small in proportion to the amount flowing through it7.
Although specific resistance is widely used as a shorthand
method of describing how well a sludge will dewater, Karr and
Keinathg noted that this test does not predict other characteristics
essential to good dewatering, such as pick-up and release
characteristics, shear resistance, and scrolling properties. For
example, an activated sludge with a very low specific resistance may
in fact be intractable, whereas a highly resistant anaerobic sludge
may handle very easily.
Compressibility
The compressibility of a sludge affects its response to vacuum— or pressure filtration. By measuring the specific resistance at
a
different pressures, the coefficient of compressibility can be
determined. It is defined as the slope of the line obtained when the
11
logarithm of the resistance is plotted against pressure:
log r = Solog P + constant [12]
An incompressible material has a coefficient of compressibility of
zero. Increasingly compressible materials have higher coefficients
of compressibilityö.
Blinding
The equations used to develop the concept of specific resistance
presuppose a straight line relationship between t/V and V. when
graphed according to this relationship, actual laboratory data often
produce a curve rather than a straight line. Notebaert5 suggested
that this nonlinearity occurs when the combined resistance (RC + Rm)
of sludges with heterogeneous particle distributions changes during
the course of filtration. Medium resistance changes when small
particles (equal in diameter to the medium pore diameter) lodge in
the pores of the medium, resulting in blinding. The rate of media
clogging decreases as the cake builds up and small particles are
retained in the cake itself (Figure 1b). Cake resistance changes
when small particles lodge in the pores of deeper layers of ‘the
filter cake, causing blinding of the cake itself. If these small
particles are larger than the pore size of the medium, specific
resistance tends to increase with time of filtration (Figure 1c).
The redistribution of particles results in deformation and
compression of the cake.
12
In order to model the resultant curvilinearity, r is redefined
as r':
r'= r (V)X [13]
Substituting, Equation_6 becomes:
dV = PA [14]— ;"—T—Tdt prw(V/A) 1+X
Integrating Equation 14 yields:
T = urw [15]
Taking the logarithm of both sides, Equation 15 becomes:
log T = lo (prw) + (2+x)log V [16]
which can be plotted as a line of the form
log T = log a + (2+x)log V [17]
where a is the average specific resistance.
The value of (2+x) can be used to characterize the response of a
given sludge to filtration. Notebaertß found that sludges with x
greater than or approximately equal to zero were more compressible,
with coefficients of compressibility of about 1. Sludges with values
of x less than zero were less compressible, with coefficients of
compressibility of about 0.3 to 0.5.
13
Huangg derived a similar concept from examination of specific
resistance data. He replaced the "x" in Notebaert's equation with 6
(the blinding coefficient), where 6 is related to change in cake
resistance which develops as cake deposition proceeds. Equation 15
can be transformed by replacing x with 6 and taking the logarithm of
both sides:
ln t = (6 + 2)ln V + ln (2pw) [18]IW?/—\
Blinding sludges (more compressible) have values of 6 greater
than zero. This corresponds to a slope of (2 + x) greater than 2 in
Notebaert's discussion. For perfectly incompressible sludges, B
equals zero. For sludges which do not resist filtration, 8 equals
-16.Karr and Keinathg approached the problem of blinding sludges by
comparing specific resistance values obtained at different solids
concentrations for a given sludge. The Blinding Index (BI) was
defined ix) range frmn zero (unblinded) to 100 percent (completely
blinded). It is defined as:
BI = 100(”1’”2) 62 [10]'T @1)
where rl and r2 equal the specific resistance values determined at
initial solids concentrations cl and c2, respectively.
For an unblinded sludge, the two specific resistances would be
equal, and thus BI = 0. For a completely blinded sludge, the two
I 14
terms are inversely equal. Their product is equal to 1, and thus BI
= 100. The validity of the relationship hinges on the dependence of
the specific resistance of a blinding sludge on solids concentration.
The Blinding Index is cumbersome, requiring two specific resistances
at differing solids concentrations.
The Relationship of Particle Size and 0ther Particle
Characteristics to Specific Resistance
The relationship between specific resistance and the particulate
structure of the sludge cake formed upon filtration was discussed by
Gale in 19677. He based his derivation upon the Kozeny equation:
r* = KSO2(1—e) [20]egpp
where
r* = specific resistance
K = Kozeny constant, or parameter
S0 = specific surface area of the particles
e = fractional voidage of the bed
pp = particle density.
The specific surface area, SO, is inversely related to the
equivalent diameter of° the particles in the sludge cake. As the
diameter of the particles increases, SO decreases. As can be seenfrom Equation 20, as SO increases (signifying a decrease in particle
15
size), r* increases as well.
This is, of course, based on the premise that the voidage
remains the same with changes in particle size. Gale noted that, in
fact, flocculated sludges often produced filter cakes of lower solids
content. The lower solids content resulted in a higher voidage and
thus even lower specific resistance. 0n the other hand, particle
compression during filtration would result in lower voidage and thus
higher specific resistance.
According to Equation 20, increases in particle density would
result in decreases in specific resistance. Gale noted that
increases in particle density would correspond to decreases in the
numbers of particles per unit. weight of solids. This decrease
would result in a decrease in the surface area across which filtrate
must flow. An increase in the weight of aggregates of particles,
i.e., floc density, might not correspond, however, to an increase in
particle density. Aggregates might grow in size without increasing
on a weight per mL basis. Thus, it is not surprising that Knocke and
Wakelandlo found that specific resistance did not vary consistently
with floc density.
Gale speculated that the presence of fines in a sludge increased
specific resistance by increasing the specific surface area and
reducing cake voidage. Research by others suggested that dilution
promoted release of fines. Roberts and Olssonll discovered that_
dilution of low solids activated sludge resulted in increased
capillary suction times (CST‘s). Ademiliuyilz found that specific
16
resistance increased with dilution of domestic sludge to about 2
percent and then decreased, while resistance of piggery and water
treatment sludges decreased with dilution to 4 and 3 percent,
respectively, and then increased.
Roberts and Olssonll found that the polymer dose for low solids
activated sludge depended upon the concentration of colloidal
particles. Similarly, Knocke and wakelandlo, finding that changes in
specific resistance with specific surface area were slight for poorly
dewatering biological sludges, suggested that conditioning dose for
these sludges was dependent upon the concentration of biopolymer in
the sludge.
The results of research reported by Karr and Keinathg showed
that changes in specific resistance with mixing, storage time, pH and
conditioning could be attributed in large part to corresponding
changes in particle size distribution. In these experiments, samples
of raw, activated, and anaerobically digested sludges were
reconstituted to approximately equal fractions of different size
ranges of particles. Buchner funnel tests were then conducted on the
samples.
In general, Karr and Keinath found specific resistance values
were closely related to particle size distribution. The relative
size of the supracolloid fraction (composed of particles of diameters
between 1 and 100 microns) determined how well a sludge would
dewater. The lower this fraction, the lower the characteristic
sludge specific resistance. Exceptions were attributed to different
17
distributions within particle size fractions, changes due to storage
durng testing, measurement errors, and other factors.
These results point out a main defect with utilizing Equation 20
for characterizing the filtration response of heterogeneous sludges:
that is, that the effective diameter, or other measures of inean
particle or floc size, can represent distributions of widely varying
shapes and physico-chemical characteristics. Representative measures
of floc or particle size (such as mean diameter) may not suffice in
predicting changes in specific resistance.
FREEZE-THAW PROCESSES
There are three main types of freeze-thaw processes used to
condition sludges: natural, indirect—contact, and direct—contact.
Natural processes depend upon extended periods of cold weather to
freeze sludge exposed in beds or lagoons. Indirect—contact processes
rely upon contact between sludge and a refrigerant across a heat
transfer surface. Direct-contact processes promote unmediated
contact between sludge and refrigerant. Direct-contact processes
include those in which water freezes in intimate contact with an
evaporating refrigerant as well as those in which solid gas hydrates
are formed.
Direct-contact processes are limited by certain authorsl3’l4 to
those in which freezing occurs as the result of water evaporation at
reduced pressures. These sources may refer to those processes using
18
an immiscible refrigerant as “indirect" freezing. In the current
study, processes which involve intimate contact between sludge and
any refrigerant, water vapor or secondary refrigerant, are classed as
direct-contact processes. Indirect-contact processes are those which
do not involve intimate contact between sludge and freezing agent.
Natural Freeze-Thaw Conditioning
In climates where freezing temperatures predominate for
prolonged periods, sludges exposed in beds or lagoons freeze slowly
and completely. Upon thawing, these sludges show much improved
dewatering characteristics.
Canfield and Sutphinlß described the results of natural
freeze-thaw conditioning of alum sludge from a high-rate direct
filtration plant in Onondaga County, New York. The sludge was
lagooned at 18-inch depths, and the supernatant drained off
regularly. After freezing and thawing, the solids content of the
decanted sludge increased from 8 to 25 percent. The product texture
varied from powdery to granular.
Bishop and Fultonlö reported the results of natural freeze-thaw
conditioning of alum sludge from a treatment plant near Rochester,
New York. Solids content increased from approximately 6 percent for
unfrozen lagooned sludges to 17 percent for frozen and thawed
sludges. The product sludge dewatered quickly when placed on a sand
filter.
In a study reported by Penman and Van Esl7, anaerobic sludge in
19
winnipeg, Manitoba, was settled throughout summer and fall in lagoons
to depths of 2 feet. The supernatant was drained off regularly.
Ouring winter, sludge was pumped into the lagoons to depths of 8
feet. Throughout the following spring, summer and fall, the thawed
supernatant was returned to the plant and the beds allowed to lie
dormant. They were allowed to freeze again the following winter.
Subsequent thawing produced a sludge with a solids concentration of
about 20 percent, suitable for land application.
Tilsworth gt_al.l8 reported the results of natural freeze—thaw
conditioning of extended aeration sludge in College, Alaska, where
freezing conditions prevail three to four months a year. Sludge
placed at 6-inch depths froze in about 3O to 50 days. Once the
sludge thawed, solids content increased by 225 to 920 percent, The
product was granular, had little odor, and was easy to transport and
place. a
In experiments in Ely, Minnesota, and Cincinnati, Ohio, Farrell
gt__al.19 found that complete freezing of alum wastewater sludge
increased initial dry solids content and improved specific resistance
(from 2.1 to 9.5 percent, and from 104 to 3.43 x 1011 m/kg).
Reed gt__gl.20 developed a sludge-specific equation for
predicting the total depth of sludge which could be conditioned by
exposure to subfreezing temperatures, based on application of sludge
in 8-cm layers. The method was verified by field applications in9
Hanover, New Hampshire, and from comparison with historical data from
Duluth, Minnesota.
20
Indirect-Contact, Freeze—Thaw Conditioning6
Indirect-contact, freeze-thaw conditioning processes rely on an
intermediate surface to transfer heat ebetween the sludge to be
conditioned and aa circulating refrigerant. The refrigerant either
has a large heat capacity, enabling it to absorb heat from the sludge
at high rates with no phase change (e.g., glycol or brine) or it
vaporizes during the process, absorbing the heat of vaporization from
the sludge.
Full- and pilot-scale indirect—contact processes for
conditioning alum water sludges at two plants in England (at Stocks
and at Fishmoor) were the subject of a number of articles in thel960's2l”23. The process at the Stocks water treatment facility
consisted of slowly freezing sludge at I5OF in 150·gallon tanks.
Compressed ammonia was pumped through 480 3/4-inch—diameter vertical
pipes immersed in the sludge. The liquid ammonia flowing through the
pipes vaporized as it was warmed by the sludge. The heat required to
warm and vaporize the ammonia was drawn from the sludge, causing the
sludge to freeze. In order to make the process economical, sludge
and ammonia were cooled prior to the freezing step by heat exchange
with the frozen product. Latent heat recovery minimized condensing
requirements and also thawed the frozen sludge. The operation was
performed in batch, with approximately 90 minutes required for
freezing and 45 minutes for thawing. The plant at Stocks processed
33,000 gpd of sludge. Prethickened sludge drained to 60 to 70 percent
solids after freezing.
21
Although the process resulted in a more easily handled product
and a °large increase in solids concentration, the systeni suffered
certain drawbacks. The main problem was the high cost of
construction and maintenance. Also, the repeated cycles of freezing
and thawing placed great strain on the tanks, which required frequent
repair or replacement. g
Indirect freezing of alum water treatment sludge was
investigated in the laboratory for the Milwaukee Sewerage
Commission24’25. In a bench-scale study, alum sludge was poured into
tall, thin rectangular pans, to depths of 1/2 to 2 inches. Contact
with circulating glycol or brine at operating temperatures of between
5 and 25OF froze the sludge in batch operations lasting from 20 to 60
minutes. Vacuum filtration produced a sludge cake of 67 to 75
percent solids from prethickened sludge. The same sludges without
treatment produced sludge cakes of 18 to 21 percent solids. The
encouraging results obtained in the laboratory led to a feasibility
study for· a pilot plant for the Milwaukee Sewerage Commissionza.
Activated sludge was to be frozen at 1/2—inch depths in pans on a
conveyer, in contact with chilled brine for 100 minutes. However,
cost analyses showed that the estimated expense of the system was too
great, and the pilot study was never implemented.
Direct-Contact, Freeze-Thaw Conditioningh
Much of the research and development of direct—contact,
freeze-thaw technology was conducted in the 1950's and 1960's under
22
the sponsorship of the Office of Saline water Research. Brianl3 andBarduhnzö published excellent reviews on the status of this
technology in 1968 and 1975, respectively. General process
descriptions were presented by Fraser and Gibson27, Fraser and
Johnson28, and weissgg. The flow of information declined sharply
upon the demise of the Office of Saline Water Research, which was
abolished in 1974 after several years of federal budget cuts26.
Research directed towards application of direct-contact,
freeze-thaw processes to wastewater treatment and sludge conditioning
has been limited. The AVCO Corporation26’28 developed a commercial
direct-contact process utilizing Freon 114 to recover recyclabe
constituents from plating wastewater. Kahn and other researchers at
Virginia Polytechic Institute and State University30'32 conducted
experiments to investigate the feasibility of conditioning wastewater
sludges primarily with butane (some experiments were conducted with
Freon 114 as well) in direct-contact processes. Molayem and
Bardaki53 used Freon 11 in a gas hydrate process to dewater
wastewater sludges.
Direct-contact, freeze-thaw processes were developed as
comparatively efficient alternatives to evaporative techniques of
desalination. The advantages of direct-contact freeze-thaw processes
include:
- absence of a metallic heat transfer surface;— minimal scaling, corrosion, and fouling; and
23
- minimal pretreatment requirements.
Energy savings are due mainly to the absence of a heat transfer
surface. Although the latent heat of evaporation is about seven
times the latent heat of fusion, this potential energy savings is
compensated for by the fact that the freezing point depression caused
by dissolved salts in seawater (and dissolved solids in wastewater)
is about seven times the boiling point elevation28.
Because of practical limitations of equipment efficiency and
control, however, processes usually operate at temperature
differences greater than the theoretical minima set by freezing point
depression (for freezing) or boiling point elevation (for
distillation)34. Energy requirements for freezing processes are
relatively low when compared to evaporative processes because of the
small temperature differentials which drive the reaction between feed
and refrigerant. For each degree that the minima are exceeded,
distillation processes suffer a sevenfold loss in efficiency compared
to freezing processes. The closeness of the temperature differential
used in freezing processes to theoretical temperature differences is
a direct result of the absence of a heat transfer surface26.
Because the processes are carried out at low temperatures,
scaling and corrosion are rare. The lack of a heat transfer surface
results in fouling being confined to reactor walls. In turn, the
absence of the potential for scaling, corrosion, and fouling
precludes the need for pretreatment.
24
These advantages are offset by two disadvantages. First,
refrigerants are expensive and removal to acceptable levels can be
difficult to achieve. Second, scale—up of desalination processes is
limited by the availability of efficient compression equipment
required to recover spent refrigerantlg.
There are three types of direct-contact, freeze-thaw processes:
- vacuum freezing, vapor compression processes;
- secondary refrigerant processes; and
- gas hydrate processes.
In the discussion that follows, feed and solution are used as
general terms to include seawater, wastewater, and sludge.
Vacuum Flash, Vapor Compression Processes - In vacuum flash,
vapor compression (VFVC) processes, precooled solution is fed into a
vacuum chamber where conditions are nmintained slightly below the
triple point of water. At this point, water evaporates and forms ice
simultaneously. The heat of vaporization is about seven times the
heat of fusion; thus, under ideal conditions, seven pounds of ice are
formed for every pound of vapor released.
The process has certain serious disadvantages. It requires
large mechanical compressors to condense the water vapor produced,
and a great deal of space. High volumes of low pressure water vapor
must be handled, with a pound of water vapor occupying 4600 cubic
feet at the operating pressure. To overcome some of these
25
difficulties, a variation of this process--—the vacuumg freezing
ejector process--·was developed. In it, ejectors replace some of the
compressors. The process is complex and both the original and the
variation suffer from large size and low efficiencyzg.
Several commercial VFVC desalination pilot plants were
constructed and installed in the United States and Israel during the
1960's, by Colt Industries and the Carrier Corporation. These plants
produced up to 240,000 gallons of fresh water from sea water daily.
By 1975, however, none of the U.S. plants were operating due to
various process and mechanical deficiencesl3’26’35.
Application of the VFVC process to treatment of paper pulp mill
effluent for dissolved solids and biochemical oxygen demand (B00)
reduction was suggested by Johnson in 196935. However, a review of
the literature uncovered no reports of utilization of this process
either for treating wastewater or conditioning sludge.
Secondary Refrigerant Processes - Secondary refrigerant freezing
processes rely on intimate contact between the solution to be
treated---the "primary" solution---and an agent with a low boiling
point at ambient or near ambient pressure---the "secondary"
refrigerant, introduced specifically for the purpose of heat
transfer. Initially developed as desalination technology, secondary
refrigerant processes have been applied in commercial ventures for
wastewater recovery. In addition, several research studies on the
effectiveness of secondary refrigerant processes have been
documented.
26
Process Description - In secondary refrigerant freezing,
precooled solution is fed into a reactor where it is intimately mixed
with an immiscible refrigerant. Conditions in the reactor are
maintained such that the refrigerant boils at 61 temperature lower
than the freezing point of water. As the refrigerant evaporates, it
absorbs the heat necessary for vaporization from the solution,
freezing the water.
A typical process diagram for secondary refrigerant desalination
is presented in Figure 227. The process comprises four unit
operations:
- heat exchange,
- freezing/crystallization,
- washing, and— melting/condensing.
These are discussed in further detail below.
Heat exchange - Feed is precooled prior to ·freezing by
contact with the ice slurry and waste concentrate produced
during desalination. Precooling avoids the use of
excessive amounts of refrigerant to lower temperature of
feed to process freezing levels._
Freezing/Crystallization - Precooled feed and liquid
27
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28
refrigerant are pumped into a reactor (crystallizer) under
pressure conditions such that the evaporating temperature
of the refrigerant is lower than the freezing temperature
of the feedlg. The refrigerant evaporates when it comes
into contact with the feed, lowering the water temperature
below its freezing point. Pure ice crystals (approximately
200 microns in diameter) form, excluding all other
· material, including solute and particleszö. The reactor
contents may be mixed by the turbulence created by
evaporating refrigerant; additional agitation may also be
provided.
Washing - The slurry from the reactor containing a mixture
of pure ice crystals and concentrate is washed, removing
the concentrate from the ice.
Melting/Condensing - Spent refrigerant vapors undergo two
compression stagesl3. Primary compression raises the
temperature of the vaporized refrigerant to the melting
point of ice. The vapor is pumped to the melter/condenser,
where it condenses in contact with the product slurry.
However, not all of the vapor can be condensed on the
product, due to incomplete heat exchange, heat leaks into
the system, and the work input of compressors, pumps, and
agitators. Some of the vapor is thus compressed to a
29
higher pressure to be condensed at a lmgher temperature
with cooling water.
In adapting the secondary refrigerant process for sludge
conditioning, the washing step is usually omitted as the object of
conditioning is not to produce pure water, nor to recover
concentrate, but to take advantage of the irreversible changes which
occur during freezing.
Thermodynamics and Kinetics of the Process — Discussions of the
thermodynamic principles involved in freezing processes have been
presented by Dodge and Eshayagö, Gilliland37, and wiegandtgg.
The minimum amount of theoretical reversible work necessary to
separate fresh water from seawater (or other solution) depends upon
the temperature of the process and the percent conversion attainedgö.
For example, the minimum amount of work required to separate 1000
gallons of fresh water from 2000 gallons c¤’ a 3.5 percent saline
solution at 2500, (a 50 percent conversion or recovery rate), is
variously calculated to be from 2.89 kw—hr to 4.15 kw-hr36’37’39. In
analyzing a continuous system in which the product water is in
equilibrium with the final concentrate alone, the minimum work rises
to 5.8 kw-hr/1000 gallons.
Although the work of separation is nnnimized at low recovery
rates, the work of pumping the feed through the process approaches
infinity as the yield of fresh water approaches zero. For example, to
recover 1000 gallons of fresh water at a 50 percent recovery rate
30
requires pumping 2000 gallons of solution. To recover 1000 gallons of
freshwater at a 0.5 percent recovery rate requires pumping 200,000
gallons of solution. At about a 50 percent recovery rate, the
pumping work becomes minimal with respect to the work required to
separate the fresh water from the solution, and this is the reason
the recovery rate is typically selected as 50 percent.
Although the amount of heat required to freeze and thaw an equal
amount of seawater are approximately the same, additional energy is
required for freezing because the freezing point of seawater is
depressed by salts below the melting point of the pure ice formed.
The minimum reversible work required by freezing processes depends
upon the freezing point depression, the process and ambient
temperatures, and the latent heat of fusion. It can be calculated
from the following equation:
w = 0 (Tl — T2) TO [21]
whereT2 T1
0 = heat of fusion
Tl,T2 = freezing temperature of pure water
and seawater, respectively
TO = ambient temperature.
work is required to pump the heat of fusion from the depressed
freezing temperature of the solution to the freezing point of water
and to discharge the heat from the work of pumping to ambient
31
temperature. The amount of minimum theoretical work required for 50
percent recovery from a 3.5-percent saline solution is approximately
6.3 kw-hr/1000 gallons of fresh water produced. However,
irreversible effects in actual processes raise the theoretical work
requirement to 40 kw-hr/1000 gallons, or more. These effects include
pressure drops from fluid friction and from throttling, heat leaks
into the system, and finite temperature and concentration gradients,
among others36.
Optimum temperature and pressure conditions for secondary
refrigerant processes depend upon the vapor saturation curve of the
refrigerant and the liquid-solid curve of the solution to be frozen.
A pressure is selected at which the temperature of the point on the
vapor saturation curve is below the freezing temperature of the
solution. The difference between these two temperatures is the
driving force of the reaction. y
The heat of' vaporization of butane (165 Btu/lb) is slightly
greater than the heat of fusion of water (144 Btu/lb). Theoretically,
1.15 lb of ice should form when water is contacted with 1 lb of
butane. In practice, refrigerant requirements are increased by
insufficient precooling of feed, incomplete mixing, and other
factors.
Process History — Several types of refrigerants have been used
in secondary refrigerant freeze-thaw processes, including butane andU
certain halogenated halocarbons. The attractiveness of butane as a
secondary refrigerant is that its boiling point at ambient pressure
32
is just below the freezing point of water. It also has a low
solubility in water, varying from 70 mg/L at 250 to 150 mg/L at 000.
At the temperatures maintained in secondary refrigerant processes, it
does not form gas or liquid hydrates. Finally, butane is relatively
inexpensive when compared to other refrigerants.
The major disadvantage of butane processes is poor refrigerant
recovery. Although relatively insoluble in water, liquid butane
tends to emulsify in impure solutions. Carryover of liquid butane in
slurry processes has been reported to vary from 1 to 10 g/L, and it
is estimated that freeze-thaw products may contain emulsified butane
concentrations up to 10 times the concentration of dissolved butane
in freeze-thaw products26. Loss of butane associated with the
product is not only expensive, but may prevent reuse or complicate
disposal of the contaminated product.
Various separation techniques which have been used to remove
butane from freeze-thaw products include stripping under vacuum and
at atmospheric pressure; stripping using vacuum sprays and packed
columnszö and charcoal filtration following vacuum strippinglg.
Application of any such separation method obviously increases the
overall cost of the process.
A secondary disadvantage of butane is its potential for
explosion at ambient temperature in the presence of oxygen. This
explosion hazard requires special consideration in the design of the
mechanical systems used for secondary refrigerant freezing and also
increases process cost.
33
Halogenated derivatives of hydrocarbons (which are also used
extensively in gas hydrate processes) are more familiar as Freons and
Arctons, the trade names under which they are manufactured. (An
explanation of numerical designations based on formula is included in
Appendix A.) They are generally nonflammable and nontoxic, with low
solubilities in water. Their densities, which are considerably
greater than water (e.g., Freon 114 has a specific gravity of 1.54)
make them easily separable.
As a group, the halogenated hydrocarbons have several
disadvantages. Their main drawback is that they are relatively
expensive in comparison with other secondary refrigerants. Also, in
gaseous form, they are heavier than air and can create a suffocating
environment if large amounts are released in confined spaces without
proper ventilation. Certain members of this group have been the
subject of controversy in the past decade, regarding potentially
destructive impacts on the atmospheric ozone layer.
Secondary refrigerant desalination projects have been developed g
and installed worldwide. Various desalination projects utilizing
secondary refrigerant processes were undertaken by commercial
concerns in the United States in the 1960's13. Among them, Blaw-Knox
Co. and Struthers Scientific and International Corporation installed
and operated 55,000 gpd and 15,000 gpd desalination plants,
respectively.N
The Japanese desalination industry has a long history of
research and development in secondary refrigerant processes as
34
evidenced by the large number of patents issued since the 1950's.
Unfortunately, little of the research associated with these efforts
has been reported in the English scientific literature. Articles by
Nagashima and Maedaao in 1979 and Nagashima gt_al.4l in 1981 reported
on the development of pilot- and full-scale direct contact
desalination plants using horizontal reactors and butane as the
secondary refrigerant in a standard process. The pilot plant
treated 45 m3/day (12,000 gpd) seawater and the full-scale plant had
a capacity of 1000 m3/day (264,000 gpd).
The British also have investigated the potential of butane
processes for desalination. In his report on the status of
desalination technology, Barduhnzö presented brief descriptions of
two bench-scale processes developed in England. The first, developed
and tested by the British Atomic Energy Authority at Harwell in the
years 1966 to 1972, produced as inuch as 200 lt> ice/hr/ft3. The
second, operated between 1965 and 1970, by the British firm Simon
Engineering, used a shell-and—draft tube reactor to produce ice at
the rate of 150 lb ice/hr/ft3.
Sludge Conditioning - Interest in secondary refrigerant
processes as alternatives to conventional methods of wastewater
treatment and sludge conditioning followed their development as
desalination technology, with most references appearing in the
1970's. Research conducted by Kahn on direct freeze-thaw
conditioning of wastewater sludges using butane was reported in
several sources in the 1970's3O-32. Experiments were conducted under
· 35
both batch and continuous operating conditions. Batch experiments ’
took place in a plexiglass reactor, with precooled butane
(temperature = -1.4506) sparged into 1500 mL of sludge at a flowrate
of 2.7 x 10-5cfs (46 mL/min) under a 3 cm (1.2 in) Hg vacuum.
Continuous experiments took place ‘Hi a 6-inch-diameter cylindrical
reactor, with a sludge depth of 6 to 12 inches. Sludge and butane
were precooled in a heat exchange system through which chilled saline
solution was circulated. Sludge and butane were fed to the reactor
at rates of 3 to 5 mL/min and 5 to 7 mL/min, respectively, under a
vacuum<M’
7 cm (2.8 in) Hg. The greater vacuum was necessary to
ensure proper conditions for butane vaporization throughout the
reactor. Butane vapors were collected and condensed by indirect
contact with the product slurry. Two compressors in series achieved
70 to 80 percent butane recovery.
Sludges tested included waste activated sludges from one
conventional and two extended aeration wastewater treatment plants.
Selected results are presented in Table 1. Batch experiments reduced
the specific resistance of the waste activated sludge from 4.7 to 1.8
x 1014 m/kg at a detention time of 60 minutes, and increased final
solids concentration from gravity drainage from 18 percent for the
unconditioned sludge to 77 percent for the conditioned sludge. It is
interesting to note that substantial improvements in dewatering
characteristics were achieved only at contact times of 40 minutes or
more, when freezing was complete. Also, the resulting treated
samples still indicated a poor dewatering sludge as evidenced by
36
TABLE 1
SELECTED RESULTS OF DIRECT·CONTACT, FREEZE·THAW SSNDITIONINGOF WASTE ACTIVATED SLUDGES WITH BUTANE
BATCH CONDITIONING
Tota1 Butane Contact Specific % ReductionDose, Time, Resistance, in Specific
mL/L min. x 10 m/kg Resistance
0 0 4,700 ·310 10 4,000 15610 20 4,400 6
1,230 40 2,000 571,840 60 1,800 62
CONTINUOUS CONDITIONING
Tota1 Butane Contact Specific % ReductionDose, Time, Resistance, in Specific
mL/L hr. x 10 m/kg Resistance
O 0 850 ·1,500 6 220 741,500 12 200 761,500 24 180 791,500 36 100 88
37
specific resistance values in excess of 1 x 1014 m/kg.
The continuous process resulted in a decrease in specific
resistance for one of the extended aeration sludges from 8.5 to 2.2 x1013 m/kg, with an increase in final solids concentration from one
percent to 20 percent, after six hours contact time. Further
improvements in specific resistance values and final solids
concentration were noted as detention times were increased up to 36
hours.
The Crystallex process, developed and promoted extensively by
AVC0 Corporation in the early 1970's, was touted as a means of
concentrating recoverable constituents in wastewater as well as
desalinating seawater. The Crystallex process utilized Freon 114 as
the refrigerant. In the process initially described by Fraser and
Johnson28, liquid Freon 114 and feed were introduced simultaneously
as a spray over a mechanically agitated pool contained in a
horizontal reactor. (The process was later modified such that the
refrigerant was sparged into the pool from the floor of the reactor.)
The ice slurry in the reactor was maintained in a fluid state by
recirculating concentrate26’42.
Slurry, concentrate, and any remaining liquid refrigerant were
separated in a hydrocyclone. The slurry was then washed in a
pressurized counter·current wash column, from whence it flowed to a
shell-and-tube melter-condenser. Freon 114 was condensed along the
outside of the melter-condenser tube. A refrigerated cold trap was
used to separate non-condensable gases from the spent refrigerant
38
after condensation. Vacuum stripping was used to remove traces of
refrigerant from the product. Additional stripping, if required, was
accomplished at atmospheric pressure26’42’43.
The Crystallex process was used, in addition to desalinating
seawater, in projects involving materials recovery from metal plating
baths and concentration of pulp and paper wastes. Preliminary
results from the treatment of a synthetic wastewater containing
nickel, cadmium, chromium, and zinc, in a 2500-gpd pilot plant,
showed that the process could reduce metal concentration in recovered
water to less than 0.5 mg/L26’28.Kahn3O also experimented with using Freon 114 to condition
sludges; results were deemed unsatisfactory due to poor settling and
dewatering characteristics of the conditioned sludge. Katz and
Mason34 and researchers working for the Sewerage Commission of
Milwaukee24 reported poor results from their attempts to condition
sludge with liquid nitrogen, methyl chloride, butane, isobutane, and
freon (type unspecified). v
Gas Hydrate Processes - Extensive research was conducted in the
1960's on the use of gas hydrates in direct-contact freeze-thaw
desalination processes. Basic studies were undertaken by Barduhn and
coworkers at Syracuse University for the Office of Saline water (0Sw)
of the United States Department of the Interior44-53. Their purpose
was to isolate hydrate-forming agents that could be employed in
economically competitive desalination processes; their efforts
resulted in the development of several pilot plants. As for other
39
freezing processes, however, research came to a halt and pilot plants
disappeared when the 0Sw was abolished in 197426.
Similar in concept to secondary refrigerant processes, hydrate
processes appear to have potential for use in wastewater treatment
and, specifically, in sludge conditioning. The technology is
virtually identical. Yet scant research has been conducted in this
area. Research on utilization of gas hydrate processes for sludge
conditioning has been limited; only. one study by Molayem and
Bardaki33 could be found via traditional literature review methods.
Gas hydrates are nonstoichiometric compounds of gas and water
characterized by a clathrate or cage structure. Molecules of gas or
gas mixtures known as "guests" inhabit a "host" crystalline lattice
of pure water54. The crystalline structure is maintained by hydrogen
bonding between water molecules and by Van der waals attraction
between host and guest55. The physical interactions between the host
and guest are relatively weak. Once the hydrate is formed, however,
the molecules of gas are trapped and cannot escape until the host
lattice breaks down54.
In desalination hydrate processes, salt-free hydrate crystals
are induced to form from seawater, then separated and decomposed to
form pure water and hydrating agent. The hydrating agent is then
stripped from the product water.
Hydrate Structure — The composition of gas hydrates has been
studied since the early 1800's. According to Cady55, the models
generally accepted today were elucidated in the 1950's by
40
M. von Stackelberg, w. F. Claussen, and L. Pauling and R. E. Marsh.
There are two structural types of gas hydrates (denoted as Type
I and Type II) consisting of 46 and 136 water molecules,
respectively. The Type I structure (Figure 3a) consists of two
pentagonal-dodecahedral cavities and six tetrakaidecahedral cavities,
with radii of 0.29 and 0.46 nanometers (nm), respectively. Corners
of the cavities are formed by hydrogen bonding of one corner oxygen
atom to an outside oxygen atom and three other corner atoms54. A Type
I hydrate (composed of 46 water molecules), can theoretically
encompass eight molecules of a hydrate—forming agent "X" with
diameter less than or equal to 0.58 nm. Thus, its theoretical
composition can be expressed as X8(H20)46, or X(H20)7•6.Experimental data show that molecules filling the small cavities
rarely exceed 0.5 nm in diameter, whereas the large cavities are
filled by molecules with diameters between 0.5 and 0.56 nm55.
The Type II structure (Figure 3b) consists of sixteen
pentagonal-dodecahedral cavities and eight hexkaidecahedral cavities,
with radii of 0.24 and 0.345 nm, respectively. The small cavities
are identical to the small cavities in the Type I structure. The
larger cavities accommodate molecules of 0.56 to 0.66 nm diameter.
If all twenty-four cavities of the 136-water—molecule framework are
occupied, the composition of the hydrate is X24(H20)136, or
X(H20)5•66. If only the larger cavities are occupied, the
composition is X8(H20)l36, or X(H20)l7.
41
OÜäüß}'Ü /'
·0*ghnvgyä
~
—
TYPE 1 HYORRTE
lf\ _ '.
' jf \$?$
·TYPEII HYORFITE~
FIGURE 3. TYPE I HNO TYPE II GHS HYORRTE STRUCTURES( FROM BERECZ. E. HNO BFILLFLFICHS. M. ( S1! 1
42
Experimental data on hydration numbers (the number <yf water
molecules per gas molecule) for both Type 1 and Type 11 structures
show considerable variation from these ideal compositions56. In
fact, it is normal for approximately ten to twenty percent of the
cavities to be unoccupied, thereby raising the water-to-hydrating
agent molecular ratio54. The fractional occupancy of a hydrate is
also affected by temperature, pressure, and the size of the guest
molecule.The bond angles and bond distances between water molecules in
both Type 1 and Type 11 hydrate structures are similar to those
between water molecules in liquid water. The hydrogen bonds are
approximately one percent longer, and the bond angles differ from
tetrahedral ice angles by 3.7 degrees in Type 1, and 3.0 degrees in
Type 1157.
Approximately thirty-five gases form hydrates with Type 1
structure; there are about sixty-five gases which form Type 11
structure hydrates57. Although there is a wide diversity in the
gases which form hydrates, they share certain common characteristics.
The shape and size of the molecules conform to the cavities in the
hydrate framework. The compounds are also typically homopolar, with
low solubility and high volatility. They experience moderate Van der
waals forces54.
Thermodyamics and Kinetics of the Process — The initial
conditions of hydrate formation (which occurs only if a hydrating
agent is present) are determined by the nature of the hydrating gas,
43
the state of the water, the pressure, and the temperature. These
conditions are best described by heterogeneous phase plots of
pressure vs. temperature, such as the generalized phase diagram from
Berecz54 shown in Figure 4. The curves depicted are:
I - the vapor pressure curve of the hydrating agent
saturated with water;
II — the vapor pressure curve of the hydrate;
III - the melting point curve of the hydrate; and
IV - the depression of the freezing point of water due
to solubilization of the hydrating agent in
water.
The hydrating gas exists in hydrate form in the regions to the upper
left of curve II and left of curve III.
Each gas hydrate is characterized by a quadruple point; that is,
a temperature and pressure at which ice, gas hydrate, liquid (or
solid) hydrating agent, and gaseous hydrating agent are in
equilibrium. This temperature and pressure are known as the critical
or decomposition values for the hydrate. This point (pk,l) is also
the pressure and temperature at which the vapor pressure of the
hydrate and the hydrating agent are equal. If the hydrate is
partially occupied, this point will occur at lower temperatures and
pressures54.
According to Davidson57, the lattice stability cyf the hydrate
44
III
I
ä Pai
_III
/1////
N
TEHPERFITURE
FIGURE 9. GENERRLIZED GHS HYDRHTE PHHSE DIHGRFIH( FROM BERECZ ( 51) 1
' 45
structure depends upon the degree <yf cavity occupancy. Since the
relative locations of guest and host molecules are known, the
fractional occupancy of the hydrate structure can be modeled using a
molecularly based, statistical theory of ideal localized
adsorption58. Cady55’56 has modeled the fractional occupancy of Type
I hydrates using a Langmuir-type adsorption isotherm equation.
Longer range interactions, asymmetry in gas—water interactions, and
restrictions of rotation and vibration of gas molecules in hydrate
cavities also must be considered, but are not usually specifically
addressed in simplified models.
John et_gl.59 addressed second neighbor effects and smoothing of
cavities due to asphericity of guest molecules. According to John
and his coworkers, stability depends upon the strength of the
physical interaction between host and guest. Thus, it follows that
the stability of a hydrate is related to the molecular size of the
hydrating agent, as attractive forces increase with increasing size.
The relationship between stability and size is proportional54.
The stability of a hydrate also depends upon the location of its
vapor pressure curve. The higher the temperature at which the vapor
pressure of the hydrate reaches 10.13 x 105Pa [145 psia), or
conversely, the lower the dissociation pressure at 006, the greater
the hyahete eteh1i1ty54.The thermal dissociation of hydrates is a four—step process54.
when the temperature drops sufficiently, the host lattice begins to
sublimate. As it does, its clathrate structure starts to
46
disintegrate. Guest molecules diffuse through the collapsing
structure, and finally desorb from its surface.
The rate of formation of a hydrate is difficult to model as the
system is complex, having two components and four phases54. It is
affected by nucleation rates, crystal growth rates, heat transfer
from the crystal to the aqueous liquid (or, in some cases, the
vaporizing hydrating agent), and mass transfer of salt or other
impurities away from the solid-liquid interface50.
Hydrates are formed primarily at the phase boundary between
liquid water and the gaseous hydrating agent54. There are two modes
of nucleation which occur: (1) homogeneous nucleation on the surface
of dispersed liquid agent droplets, and (2) heterogeneous nucleation
initiated by crystal fracturing6O. while hydrates can form inside
the liquid on dissolved gas particles, this requires greater
activation energy to reorient the surrounding water molecules. The
high molar ratio of gas to water in the vapor phase makes hydrate
formation in the vapor region unlikely as wellöl.
Factors which have been found in laboratory studies to
significantly affect the rate of formation of gas hydrates include
- 6T, the magnitude of the process driving force; that
is, the temperature differential between the
equilibrium temperature of the hydrate at the bulk_
salt concentration and the actual bulk aqueous
temperature;
47
- the degree of agitation or power input; and
- the salt concentration50.
The driving force 6T is expended primarily for (1) processes
taking place between hydrate crystals and the aqueous phase and for
(2) heat transfer from the aqueous phase to agent droplets,
especially for vaporization of the hydrating agentöl. Although
Barduhnöl suggested that the nature of the agent molecule may have
little effect on the kinetics of' hydrate formation, the relative
demand of these two processes seems to vary with the hydrating agent
used. working with Freon 31, Barduhn estimated that two-thirds of
the total driving force was consumed by agent evaporation, and
one-third by crystal growth. In contrast, the Office of Saline water
Research reported results of earlier work with methyl bromide5l which
assigned ten to twenty percent of the driving force to the former,
and eighty to ninety percent to the latter. In the formation of
hydrates from refrigerants, the relative amount of liquid agent
present surely affects the rate of formation as its presence enhances
heat transfer through evaporation.
Agitation of the hydrate-containing aqueous solution promotes
both homogeneous and heterogeneous nucleation by renewing contact
surfaces constantly and by breaking crystals apart. Barduhn's
group6O’6l developed empirical equations relating rates of formation
of certain hydrates to the power input and to the driving force, 6T.
48
Further research confirmed the importance of power input. Barduhnöl
noted a tenfold decrease in rate of production of Freon 31 and Freon
142a crystals brought to a steady state iri a continuously stirred
vessel when agitation ceased.
Mass transfer of salt and dissolved agent has been determined to
be relatively unimportant in affecting formation rate, although
increasing salt concentration does tend to cause a decrease in
reaction rate5l.
Process History - In its annual report for 1960, the Office of
Saline water published a list of hydrate-forming agents for potential
use in desalination processes, including several Freons,
cyclopropane, methyl bromide and vinyl chloride44. A number of
agents screened did not form simple hydrates. Others were considered
impractical because of their relatively high decomposition pressures.
In 1961, the OSN published a revised list of the most promising
agents for use in desalination45. Chlorine, methyl chloride, Freon
12, and propane had been added to the list, while cyclopropane, Freon
12B2 and vinyl chloride had been dropped.
This initial research on hydrating agents specifically suited
for desalination was carried out by Barduhn and coworkers44’45. Over
the next twenty years, they produced a considerable body of
thermodynamic and kinetic data for many of these agents, including
Freons 12, 21, 31 and 142b46’48’5l-53’6l. inain amaria for anaevaluation of a compound as a suitable hydrating agent included
49
- moderate decomposition temperature and pressure;
— high rate of hydrate formation;
- low losses due to solubilization or hydrolysis; and
- reasonable cost.
Secondary considerations included crystal separability and
refrigerating capacity. More recent work by Kubota58 produced
thermodynamic data on Freon 13, Freon 23, and Freon 152a.
Hydrating agents of particular interest are discussed in more
detail below. Their decomposition pressures and temperatures, as
well as their hydration numbers, are given in Table 2.( Freon 12 (CCl2F2) forms a Type 11 hydrate, with an approximate
composition of Freon 12(H20)l7. It has a decomposition temperature
of 12.1OC and a decomposition pressure of 4.58 x 105Pa (64.5 psia).
Freon 12 was used to start up the Koppers Co. propane hydrate
pilot desalination plant, built for the 0Sw at wrightsville Beach
Test Facility, South Carolina, in 196650-52. Freon 12 was also
tested at the same location from March, 1967, to July, 1968, in a
pilot program conducted by the Mason—Rust Co. Efforts concentrated
on optimizing wash—separation processes rather than hydrate
formation, as Freon 12 hydrate crystals proved difficult to separate.
Production rates were low and failed to offset the high capital and
operating expenses, and the plant finally closed down for economic
reasons, although technically it worked well.
Freon 31 (CH2ClF), a Type I hydrate, has a high decomposition
50
· TABLE 2E
DECOMPOSITION TEMPERATURES AND PRESSURES OF HYDRATING AGENTS
Decompos.Decompos. Presägre, Hydration
Agegg TENE.2 °C x 10 Pa Number Bei;
Carbon Dioxide 31.1 73.73 6 54
Chlorine 28.7 6.09 7.27 45
Cyclopropane 17.1 5.96 - 44
Freon 12 12.1 4.58 17 45
Freon 1281 10.0 1.70 17 44
Freon 1282 9.9 2.68 17 44
Freon 13 8.5 24.2 19.3 58
Freon 21A
8.7 1.01 16.6 44
Freon 2281 9.9 2.68 17 44
Freon 23 19.9 40.4 7.9 58
Freon 31 17.9 2.86 8.0 44
Freon 1428 13.1 2.32 7.2 45
Freon 152A 15.3 4.51 17 44
Methyl Bromide 14.7 1.53 7.9 44
Methyl Chloride 21 5.07 7.2 45
Propane 5.5 5.67 18.4 58
Vinyl Chloride 1.2 1.82 · 44
51
temperature (17.906) and a moderate decomposition pressure (2.86 x105 Pa, or 41.5 psia). It has an extremely low hydrolysis rate and a
high rate of formation. Results of kinetic studies showed that the
Freon 31 hydrate ·formed six to ten times ·faster ‘than hydrates of
propane, methyl bromide, or Freon 1252. Crystals were granular and
easy to wash53. Unfortunately, Freon 31 is no longer commercially
available.
Freon 142b (6H366lF2) produces a Type II hydrate which
decomposes at 13.106 and 2.32 x 105 Pa. Freon 142b was used in
Barduhn's kinetic studies on the rate of formation of hydrates as
function of temperature differential44.
Propane (63H8) forms a Type II hydrate with a relatively low
decomposition temperature (5.706) and a high decomposition pressure
(5.67 x 105 Pa, or 82.2 psia). Despite these unfavorable
characteristics, it has been the subject of continued laboratory and
pilot studies because of its ready availability44’45’48°5l.
In 1960 and 1961, the results of laboratory research conducted
by Koppers Co. on a bench—scale propane hydrate desalination process
were reported44’45’48-51. Hydrate yield varied from 3 to 21 weight
percent of feed. Agitation proved critical; problems with crystal
separation were also noted.
The laboratory bench-scale work undertaken by Koppers resulted
in the design and construction of a 10,000-gpd pilot plant at the~
wrightsville Beach Test Facility, which was completed in 196648-51.
The seawater was first pretreated by filtering suspended materials,
52
chlorinating, and deaerating, and then prechilled. The seawater was
introduced into a reactor where propane was added and hydrates were
formed. Following hydrate formation, the hydrate crystals were
washed, liquid propane was decanted from the waste brine and the
product water, and the hydrate slurry was decomposed. Gaseous
propane was stripped from the waste brine and product water streams.
The ultimate failure of the pilot operation was attributed to the
poor washing characteristics of the propane hydrate crystals.
In the early 1960's, the Sweet water Development Company also
tested a propane hydrate desalination process46-48. Pilot tests were
conducted at a small scale on a 700-gpd pilot plant in St. Louis,
Missouri. The encouraging results obtained from this plant led to
the design and construction of a 20,000-gpd pilot unit at the 0Sw's
Wrightsville Beach Test Facility. The process resembled that
developed by Koppers. However, the washing operation relied on a
cocurrent displacement system which employed a cyclone to separate
propane, water, and hydrate crystals based on differences in
densities. The cyclone did not provide satisfactory performance and
was eventually replaced with a pressurized wash column.
Chlorine (Cl2) produces a Type I hydrate that has one of the
highest decomposition temperatures (28.7OC) of the group of hydrates
actively considered for use in desalination processes. Unfortunately,
it also has a high decomposition pressure (6.09 x 105 Pa or 88.3
psia), is extremely corrosive, and is highly toxic. Because of its
wide availability, however, it is still considered a potential
53
desalination agent62. No references to its use in bench-scale, pilot
or full-scale projects were found.
Carbon dioxide (CO2) has a very high decomposition temperature
(31.1OC) and a very high decomposition pressure (73.73 x 105Pa or
1069 psia). Despite its high decomposition temperature and pressure,
it is attractive as a desalination agent because it is nontoxic,
nonflammable, and readily available at reasonable cost.
In 1964, it was reported that the „Jacobs Engineering Company
investigated the use of carbon dioxide as a hydrating agent for
desalinationag. The process used multiple stages of hydrate
formation, applying the carbon dioxide step-wise to avoid flash
hydrate formation, which apparently can have the same deleterious
effects as flash freezing in freezing processes. Neither direct or
indirect use of carbon dioxide as a refrigerant was practical, and
ammonia was used for all heat transfer processes instead. Carbon
dioxide recovery was accomplished by vacuum stripping. Crystal
separation took place in a continuous classifier.
Methyl bromide (CH3Br) and methyl chloride (CH3Cl) have both
been seriously considered as hydrating agents55’58. Methyl bromide
is a Type I hydrate with a high decomposition temperature (14.7OC)
and low decomposition pressure (1.53 x 105 Pa or 22.2 psia).
Kinetic studies on rate of formation of methyl bromide hydrate
were conducted in a continuously fed, stirred vessel, and compared
favorably with other agents. Methyl bromide was eliminated from
consideration as a desalination agent, however, when it was
54
discovered that its relative cost, due to a high rate of hydrolysis,
made it economically unattractiveäl.
Methyl chloride, also a Type I hydrate, has a high decomposition
temperature (21.0OC) and an acceptably low rate of hydrolysis. Its
high decomposition pressure (5.07 x 105 Pa or 73.5 psia) has
discouraged researchers from pursuing further kinetic studies.
Sludge Conditioning - The literature search for this study found
only one reference regarding the application of the gas hydrate
process to sludge conditioning. Molayem and Bardaki33 dewatered
samples of primary and activated sludge as well as mixtures of the
two sludges with excess quantites of Freon 11. 500-mL doses of Freon
11 were applied to 20 mL samples in 10-minute stages. Sludge solids
were physically separated from Freon 11 hydrate crystals during the
course of the experiments. As can be seen from the selected results
presented in Table 3, high concentrations of final solids were
obtained in certain instances.
The practical significance of this study is questionable for the
following reasons:
1. Results were extremely variable. Percentage increases in
final solids concentration varied from 13 to 94 percent for
primary sludge; from 43 to 98 percent for activated sludge,
and from 55 to 91 percent for mixtures.
2. Estimated values were used in calculating final solids.
55
TABLE 3
SELECTED RESULTS OF DIRECT-CONTACT, FREEZE-THAWBSONDITIONINGOF WASTEWATER SLUDGES WITH'FREON 11
ONE-STAGE CONDITIONING
Initial FinalSolids, Solids,
Sludge % %
Primary 7.0 5#.0
Primary 7.0 1#.7
Secondary 1.8 #.0
Secondary 1.8 52.6
Mixture 5.3 11.5
Mixture 5.7 #0.5
TWO—STAGE CONDITIONING
Initial FinalSolids, Solids,
Sludge % %
Primary 7.# 20.3
Primary 9.3 10.6
56
Final solids concentrations were calculated from equations
which required estimates of the amount of water remaining
associated with the hydrates formed during the experiment.
3. Excessive mnounts of' Freon 11. were used in experiments.
The applied Freon dose varied from 12.5 to 25 L Freon per L
of sludge.
IMPACT OF PROCESS AND HANDLING VARIABLES ON CONDITIONING
EFFECTIVENESS OF FREEZE—THAN CONDITIONING
Factors which affect the conditioning effectiveness of
freeze-thaw conditioning processes include the rate and extent of
freezing; type, amount, and point of chemical application; length and
condition of storage; sludge solids content; and the amount and
intensity of handling and mixing. These factors are discussed in the
following subsections.
Rate and Extent of Freezing
It is generally accepted that effective freeze-thaw conditioning
of sludges is only achieved by slow, complete freezing. Studies of
natural and indirect freeze-thaw conditioning have, in general, borne
out this beliefl8’l9’34’63. Experiments conducted using secondary‘
refrigerant processes have shown that slurry freezing could also be
used to successfully condition sludges.
57
Katz and Mason34 conducted indirect freezing experiments with
waste activated sludge. They found that deep freezing caused the
solids to separate from the liquid and form layers. Rejection of
solids occurred at a critical freezing rate of 0.0005 mL/sec (0.03
mL/hr). At freezing rates greater than 0.001 mL/sec (0.06 mL/hr),
sludge particles and unfrozen liquid were trapped in the advancing
ice matrix. Rapidly frozen sludges did not dewater as well as
sludges which had been frozen at a slower rate.
In experiments to determine the relationship between freezing
speed and conditioning effects, Logsdon and Edgerly64 progressively
froze samples of barium sulfate sludge, iron and aluminum hydroxide
sludges, and alum water treatment sludge. The 350-mL samples were
placed in plastic bags and lowered into an antifreeze bath at a fixed
rate. As freezing progressed, solids tended to migrate upwards and
consolidate. The lower the freeze rate, the greater were the
migration and consolidation. Critical velocity of the freezing
isotherm was about 30 mm/hr, above which no migration occurred. Fast
freezing of iron and alum sludges resulted in local segregation of
particles. Although segregation patterns were different in frozen
samples of the two different kinds of sludge, both sludges showed
improved dewatering characteristics, as evidenced by decreases in the
equivalent volume of settled solids in settled samples.
Ezekwo gt_al.62 subjected partially digested secondary sewage
sludge to progressive freezing by lowering sludge-filled glass tubesthrough a chilled metal block. Freezing rate varied from 0.8 to 8.8
58
x 10-4 cm/sec (0.05 to 0.53 mm/hr). Although there were
morphological differences observed in cross and longitudinal sections
of sludge frozen at different rates, solids obtained upon gravity
drainage did not vary appreciably with freezing rate.
In experiments in which biological sludges were frozen by
contact with butane, ‘Khan3O and Randall, et_Jal.,32’65 found that
slurry freezing improved dewatering characteristics. In both batch
and continuous processes, increasing the contact time between sludge
and butane improved conditioning. The improvement in the specific
resistance of the activated sludge freeze-thaw conditioned in the
batch process corresponded to a first—order reaction curve,
approaching a maximum at 60 minutes. Contrary to results produced by
solid freezing, filtrate quality improved with conditioning time,
although supernatant quality decreased.
Chemical Addition
Several studies have reported that the addition of inorganic
chemicals or polymers to freeze-thaw conditioning improved dewatering
characteristics. The addition of ferric chloride to activated sludge
prior to freezing improved dewatering rates24. Preaddition of alum to
activated sludge increased solids production rate and resulted in
more efficient solids capturego, and improved dewatered solids
concentration for a variety of wastewater treatment sludges66.
Polymer addition prior to freezing also decreased sedimentation
volumes of iron and alum sludges63; polymer addition to digested
59
sewage sludge during the freezing process dramatically improved
solids migration67. In contrast, chemical addition after
conditioning has been found to hinder dewatering24.
Baskerville68 has suggested, that preconditioning with these
agents strengthens the delicate flocs which constitute some
biological and chemical sludges. The improved structure of the floc
is more able to withstand the potentially destructive pressures of
the freeze—thaw process.
Storage
Gale gt_gl;69, in their basic studies on the effects of handling
variables on the dewatering characteristics of raw sewage sludge,
found that storage of unconditioned and alum-conditioned sludges over
a period of days resulted in large increases in specific resistance.
Other researchers have confirmed that storage of sludge prior to and
after freeze-thaw conditioning generally resulted in deterioration of
dewatering characteristics. In a study for the Sewerage Commission
of Milwaukee24, samples of activated sludge stored for periods up to
24 hours, before and after indirect—contact, freeze-thaw
conditioning, resulted in deterioration of dewatering
characteristics. Khan30 observed that storage of biological sludges
both prior to and after direct-contact conditioning with butane
hindered settling, filtration, and drainage.
Doe gg_gl.22 found that the dewatering characteristics of alumsludges deteriorated appreciably after E3 to IO hours of thaw time
60
following indirect-contact, freeze-thawconditioning.Thickening
.
The effect of initial solids concentration, and, thus, the
usefulness of prethickening in freeze-thaw conditioning of sludges is
disputed. Certain studies have shown that conditioning improves with
increased initial solids concentration while others have shown the
opposite effect. This is an important consideration as prethickening
can decrease the volume of sludge freeze—thaw conditioning processes
must handle, resulting in substantial cost savings.
Doe gt_al.23 prethickened alum water treatment sludges to 2.4
and 4 percent prior to successful indirect—contact, freeze-thaw
conditioning. In 61 study conducted for the Sewerage Commission of
Milwaukee24 activated sludge was prethickened to 4 percent with no
adverse effect on the dewatering characteristics of the
indirect-contact, freeze—thaw conditioned sludge.
Katz and Mason34 found that the dewatering time of
indirect-contact, freeze-thaw conditioned activated sludge decreased
as feed solids concentration increased from about 1 to 1.5 percent to
about 2 to 2.5 percent.
Ezekwo gt_al.64 compared the solids concentration of
progressively frozen, partially digested sewage sludge after thawing
and gravity drainage. Undiluted sludge (4 percent) dewatered to a
higher concentration than diluted sludge (2.2 percent).
In contrast to these studies, Tilsworth et_al.18 reported on
61
natural freezing of extended aeration sludges, noting that the lower
the solids content of the sludge, the more efficient the process.
Randallgz, in slurry freeze—thaw conditioning of biological
sludges, also found that higher solids concentrations required longer
detention times. The relationship could be modeled according to the
equation:
YCT = axfz + 6 [24]where
YCT = conditioning timexf = feed solids concentrationa,b = constants.
Handling and Mixing
Handling and mixing have been shown to have an adverse effect on
the dewatering characteristics of certain sludges22’23’69. The
effect depends upon the type of sludge and the intensity and duration
of handling and mixing. Farrell7O noted the negative effects of
stirring on both sewage and alum hydroxide sludges which been
freeze-thaw conditioned; the effect was more pronounced for sewage
sludge. Khan30, in his direct-contact, freeze-thaw conditioning
experiments with biological sludges, found that unixing during the
freezing process was necessary to maintain a pumpable slurry.l
Vigorous agitation resulted ‘Hi a poorly settling sludge, but its
effects could be partially allayed by subsequent slow stirring.
62
MECHANISMS OF FREEZE·THAw CONDITIONING
Freeze-thaw conditioning produces irreversible changes in the
nature of some sludges, making them, in many cases, easier to
dewater. Several mechanisms have been proposed to explain these
changes. A discussion of the mechanisms involved in freeze-thaw
conditioning of sludges is difficult to approach, as various theories
put forth are based upon the extent and rate of freezing as well as
the type of sludge conditioned. Mechanisms can be roughly divided
into two categories:
- solids migration and compression, and
- particle dehydration and cell rupture.
Solids Migration and Compression
The segregation of particles and layers of particles (termed
micromigration and nacromigration, respectively, by Logsdon and
Edgerly63) which occur when sludges are deep frozen has been noted in
a number of studies. The irreversibility of the changes wrought by
freeze-thaw conditioning has led some researchers to suggest that
the forces which are responsible for segregation are large enough to
destroy cells and to compress particles and flocs, dehydrating and
concentrating them.
The behavior of solids in a freezing liquid is a result of the
process of crystallization and of the nature of the solids
themselves. Ice crystals nucleate and, if unimpeded, proceed to grow
63
in planes. If surrounded by solution, the crystal interface is
destabilized by the concentration gradient of the solute. In
response, the crystal sends out projections and loses its planar
characteristics, becoming dendritic. As the solution is dehydrated
at the ice interface, colloidal solutes lose some of their mobility.
The interface pushes‘ particles ahead of it, excluding them by
surface—energy effects. Solids thus tend to localize at the grain
boundaries of the ice crystals64’67.
whether or not a particle in the path of the advancing interface
is trapped depends upon the size and roughness of the particle, the
solids content, and the rate of crystal growth63’64’67. The larger
the particle, the lower is the velocity required to trap it. while
polymers increase the size of particles, they improve the
concentration of solids by lowering the resistance of flow through
them, thus preventing entrapment of solids. The larger the surface
area relative to particle size (i.e., the rougher the particle), the
greater is the tendency of the particle to be carried along by the
interface.
Ezekwo gt_al.64, from their work with partially digested sewage
sludge, noted differences in the behavior of samples of diluted and
undiluted sludges upon thawing. The solids from the undiluted sludge
(4 percent) formed a rigid mass which retained its longitudinal form,
collapsing along the side of the tube in which the sludge was frozen
and thawed, during melting and draining. This facilitated the flow of
water from the mass. On the other hand, the diluted sludge solids
64
formed a fragile mass which broke apart during collapse, and settling
at the bottom of the tube during melting hindered drainage.
From these observations, the researchers hypothesized that slow
freezing permitted development of elongated crystals which drained
well. Rapid freezing resulted in small ice crystals enveloped by a
matrix of dissolved and suspended solids which drained poorly.
Migration of solids was hindered by increased initial solids
content, as evidenced by decrease in the size of ice domains. The
higher the solids content, the lower the rate at which impurities
diffused in the system. At high solids concentrations (greater than
80 percent), nucleation and crystal growth were severely reduced.
Logsdon and Edgerly63, found that freeze-thaw conditioning had a
decreased effect on sludges which had relatively poor dewatering
characteristics before conditioning. They suggested that the
segregated solids formed a cake similar to that formed during the
Buchner funnel test, with ice as the supporting medium. Highly
flow-resistant sludges were inclined to entrap solids during
freezing.
Particle Dehydration and Cell Rupture
Silvares et_al.71 developed a model on freezing injury to cells
based on two effects:
— solution effects, predominant in slow freezing,
wherein cells are immersed in a concentrated salt
65
solution as ice forms outside the cell. The
concentration gradient exerts an osmotic effect upon
the water in the cell, drawing water from the cell and
thus dehydrating it.
- intracellular freezing, predominant in more rapid
freezing, wherein ice forms inside the cell.
Several researchers have suggested that freezing has a
dehydrating effect on sludge particles. As water freezes, the
unfrozen solution surrounding the crystals becomes increasingly
hypertonic. This imbalance causes cellular or bound water to duffuse
to the immediate environment of the cells or flocs. Rapid or deep
freezing causes cells and flocs to rupture, releasing their contents.
Upon thawing, the filtrate contains a higher percentage of dissolved
solids because of the material extracted from the particles3O’34.
Farrelllg speculated that freeze-thaw conditioning removed water
from hydroxide flocs, whereas its basic effect on sludge particles
was to enhance agglomeration. Sewage sludge particles were thus
susceptible to resuspension upon mixing.
Role in Direct-Contact Processes
The role of either of these mechanisms in direct contact
conditioning processes is not clear. Large scale migration of
particles is not possible in well-mixed systems in which the sludge
66
is maintained as a slurry. whether local compression and dehydration
at the ice-liquid interface is sufficent to cause the irreversible
changes noted in previous studies is not known.
67
III. METHODS AND MATERIALS
Samples of water and wastewater treatment sludges were
conditioned using a variety of methods and analyzed to determine the
relative effectiveness of direct-contact, freeze-thaw processes.
This section describes sludges, conditioning methods, equipment and
process variables, and analytical methods used in this study.
SLUDGE SOURCES
Samples of waste activated sludge, primary sewage sludge, and
alum water treatment sludge were used in this study. General
characteristics of each sludge and the handling protocols developed
for each are detailed in this section.
waste Activated Sludges
Samples of waste activated sludge from the Roanoke wastewater
Treatment Plant (Roanoke, Virginia), and from the Christiansburg
wastewater Treatment Plant (Montgomery County, Virginia) were only
used in preliminary experiments. Samples of waste activated sludge
from the Stroubles Creek wastewater Treatment Plant (Montgomery
County, Virginia) were used throughout the study.
Samples of Stroubles Creek waste activated sludge were drawn
from two sources. Sludge for same-day testing was bled through a tap
68
on the main line returning settled sludge from the secondary
clarifiers to the aeration basins. Sludge for use over the course of
several days was taken directly from the aeration basin. In both
cases, the sludge was allowed to settle and excess supernatant
decanted before transport to the laboratory. Sludge from the
aeration basin was transferred to 30—liter plastic batch reactors,
stored at 200 Celsius and aerated. Samples were withdrawn from these
basins, settled, and decanted, as needed. The batch reactors were
fed approximately 400 mg/L Bactopeptone and supernatant decanted and
replaced with tap water daily.
The initial solids concentration of the settled sludge was about
1 percent (varying frmn 0.6 to 1.6 percent). Specific resistance
values generally ranged from 4 to 70 x 1011 m/kg. Cake solids
concentrations resulting from Buchner funnel tests varied from 9 to
15 percent. Sludge characteristics remained stable over the periods
in which the sludge was maintained in the batch reactors. These
periods did not exceed four days.
Primary Sewage Sludge
Samples of primary sewage sludge were obtained from the primary
clarifier underflow lines at the Stroubles Creek wastewater Treatment
Plant. Sludge was collected during waste pumping and screened
through a 1/4-inch plastic mesh to remove fibrous materials. Samples
were permitted to settle before testing and excess supernatant
decanted.
69
Initial dry solids concentrations and specific resistance values
of primary sludge samples varied greatly. Initial solids
concentrations of the settled sludge varied from 1 to 6 percent.
Specific resistance values ranged from 80 to 7100 x 1011 m/kg, and no
cake was formed during Buchner funnel vacuum-filtration tests.
Primary sludge samples were conditioned and tested within 8 hours of
collection, as specific resistance of the sludge increased greatly
with prolonged storage.
Alum water Treatment Sludges
Samples of alum water treatment sludges were obtained from two
sources. 0ne set of samples (used only in preliminary studies) was
obtained from an industrial water treatment plant in Philadelphia,
Pennsylvania. The other set was collected from the water treatment
plant at the Radford Arsenal Ammunitions Plant (RAAP) in Fairlawn,
Virginia.
The RAAP alum sludge was drawn from the thickening tank at the
solids handling building at the plant. The suspended solids
concentration of the thickened sludge was ranged from 1 to 5 percent.
The sludge was diluted with tap water to obtain lower initial solids
concentrations when necessary.
Specific resistance values for the undiluted sludge ranged from
160 to 310 x 1011 m/kg. while cake solids concentrations resulting
from Buchner funnel tests varied from 7 to 26 percent, they generally
were between 20 and 26 percent. Specific resistance values for
70
samples diluted with tap water to about. 1 percent initial solids
concentration ranged from 100 to 160 x 1011 m/kg; cake solids
concentrations varied from 23 to 24 percent.
Storage did not appreciably affect sludge dewatering
characteristics for the RAAP sludge. Undiluted sludge settled very
slightly during storage periods of over a nmnth, and solids were
easily resuspended and stabilized by mixing. Diluted sludge settled
moderately over the course of several hours.
CONDITIONING METHODS
Four methods were used to condition samples of Stroubles Creek
waste activated and primary sludges, samples of a mixture of these
sludges, and samples of RAAP alum sludge to gauge the comparative
effectiveness of direct-contact, freeze-thaw conditioning. These
included direct-contact, freeze-thaw conditioning with butane and
with Freon 12; indirect—contact, freeze—thaw conditioning; and
polymer conditioning. The experimental matrix for these studies is
presented in Table 4. Information on conditioning agents and
equipment and process variables is given below.
Direct—Contact, Freeze-Thaw Conditioning with Butane
Sludge samples were mixed with butane under temperature and
pressure conditions conducive to the formation of ice. All
experiments were continuous. Predetermined doses of butane were
71
TABLE 4
EXPERIMENTAL MATRIX
CONDITIONING METHODIndirect Butane Freon 12Freeze- Freeze- Freeze-Thaw
Sludge Polymer Thaw Thaw Batch Continuous
Stroubles Creek X X X X XWaste Activated (WA)
Stroubles Creek X X X XPrimary Sewage (PS)
Stroubles Creek (WA/PS) X X X
RAAP Alum SIudgeUndiluted X X X X XDiIuted X X X X X
72
introduced into 1-L sludge samples at a set flow rate of 20 mL/min.
Butane was introduced into the sludge either as a pure liquid or in
the form of colloidal liquid aphrons.
The butane used in this study was "cp" grade, compressed in
30-lb cylinders, and was obtained from an industrial source. Vapor
saturation data for butane are given in Table 5. The graph of these
data in the relevant temperature range is shown in Figure 5.
Direct-Contact, Freeze—Thaw Conditioning with Dichlorodifluoro-
methane (Freon 12)
Sludge samples were mixed with dichlorodifluoromethane (marketed
as Freon 12 by E.I. DuPont de Nemours & Co., and referred to as such
henceforth) under temperature and pressure conditions conducive to
the formation of gas hydrates. Two types of experiments were
undertaken: batch and continuous. In the batch experiments,
selected doses of Freon 12 were rapidly introduced into 1-L sludge
samples at pressures too high for hydrate formation. The sample and
the refrigerant were mixed vigorously and the pressure lowered to an
appropriate level for hydrate formation. Certain samples were
subjected to repeated slug doses of Freon 12 for two- and three-stage
conditioning. In the continuous experiments, predetermined doses of
Freon 12 were introduced into the sample continuously at a set flow
rate of 10 mL/min, at temperatures and pressures suitable for hydrate
formation.Freon 12 was obtained compressed in 30-lb disposable jugs from a
73
TABLE 5
BUTANE VAPOR SATURATION DATA
English Units _ SI UnitsT€|T\p€|'atU!‘€ Pressure T€IT|p€|‘ötUf'€ P|'€SSgf'8
°F gsia °C x 10 Pa
0 7.30 -18 0.5035 8.20 -15 0.565
10 9.21 -12 0.63515 10.33 -9 0.71220 11.56 -7 0.797
25 12.90 -4 0.88930 14.35 -1 0.98931.1 14.70 -0 1.01335 15.95 2 1.10040 17.62 4 1.215
74
80
§_20LJ1DLDLDääO- 10
0 0 10 20 30 40TEMPERFITURE. ° F
1.5
IIL1E, 1.0•-I
><LJ1äUJ 0.5LLI10.
0.0-18 -18 -7 -2 4TEMPERRTURE. °C
FIGURE S. BUTHNE VHPOR SRTURRTION CURVE.
75
commercial source. Vapor saturation and gas hydrate eguilibrium data
for Freon 12 are given in Table 6. Graphs of these data in the
relevant temperature range are shown in Pigure 6.
Indirect-Contact, Freeze-Thaw Conditioning
Indirect-contact, freeze-thaw conditioning was used to estimate
the maximum potential response of each sludge to other freeze-thaw
processes. Indirect freezing of sludge samples was accomplished by
placing samples in a conventional deep—freeze unit and allowing them
to freeze completely. Two-liter samples initially at room
temperature when placed in the unit cooled to o°c in two hours, and
froze completely in 24 hours. Completely frozen samples were removed
from the unit and thawed at room temperature to approximately 2000
before analyses were performed.
Polymer Conditioning
Results of polymer conditioning were used as a conventional
standard against which results of freeze-thaw conditioning were
compared. Samples of sludge (volume = 500 mL) were dosed with
varying amounts of a 0.1-percent solution of Betz 1160, a high—weight
cationic polymer, in a standard jar test apparatus. Samples were
mixed at 100 rpm for approximately 10 to 15 seconds, and then
flocculated for 30 to 60 seconds at 40 rpm.
76
TABLE 6
FREON 12 VAPOR SATURATION AND GAS HYDRATE EOUILIBRIUM DATA
VAPOR SATURATION DATA
English Units SI UnitsTemperature Pressure Temperature Pressgre
°F gsia °C x 10 Pa
10 29.33 -12 2.02215 32.42 -9 2.23520 35.74 -7 2.46425 39.31 -4 2.71030 43.15 -1 2.975
35 47.26 2 3.25940 51.67 4 3.56245 56.37 7 3.88750 61.39 10 4.23355 66.74 13 4.602
HYDRATE EOU|LlBRIUM DATA
English Units SI UnitsTemperature Pressure Temperature Pressgre
°F gsia °C E x 10 Pa
33.4 6.38 0.8 0.4435.6 7.83 2.0 0.5437.0 8.85 2.8 0.6137.6 9.57 3.1 0.6638.7 10.88 3.7 0.75
39.9 13.20 4.4 0.9141.7 15.52 5.4 1.0743.2 18.27 6.2 1.2644.4 21.17 6.9 1.4645.1 22.92 7.3 1.58
45.9 25.82 7.7 1.7846.8 28.14 8.2 1.94 _48.4 35.24 9.1 2.4349.6 41.04 9.8 2.8351.6 42.49 10.9 2.9352.9 60.62 11.6 4.1853.4 64.25 11.9 4.43
77
75Ü VRPÜR SGTURRTIÜN l® HYDRQTE EGUILIBRIUM il]
Y 0
äso u“
Q E 5 0; °L?} Y 0ua , YEIla25 dy
99_9.g=°
6 9
010 20 30 40 50 60TEMPERHTURE,%”
SE VHPÜR SGTURGTIONO HYÜRGTE EGUILIBRIUME __ =
E 4 9”
•-4 ·,X g
A
LJ _, 5 0; ”Q «•
ä P 55 0;U) 2 II ,0;L•J '·Q: 0:4O. _9
6 9,0%%
L: ’•‘
0-12 -3 G 15TEMPERHTURE,T
I-'IGURE S. FREDN 12 VRPOR SRTURFITION BND GHSHYDRFITE EQUILIBRIUM CURVES.
78
EXPERIMENTAL APPARATUS
The experimental apparatus used in the experiments conducted as
part of' this study is shown schematically in Figure 7. The nmin
components of the system were the reactor, heat exchange systems, and
refrigerant feed systems, which are described in detail in this
section.”
Reactors
The original reactor used in this study was constructed of
I/4—inch-thick Plexiglas. It had a rectangular 6-inch by 10-inch base
and 8-inch side walls. The reactor base had an integral diffuser
composed of shallow I/8—inch-wide channels grooved between two layers
of Plexiglas. The channels were laid out iri a rectangular grid.
Tiny holes (I/32-inch in diameter) were drilled through the top layer
of the Plexiglas base to allow liquid refrigerant to bubble up from
the channels into the reactor.
The reactor was fitted with a sealed cover. The cover included
several ports for vacuum and temperature gauges and for a line
through which a vacuum could be drawn and maintained. The cover also
had a removable plate fitted with a bearing for a mixer shaft.
Trial experiments using water proved the reactor configuration
to be inadequate. Ice formed directly over the diffuser, and mixing
was neither sufficiently intense nor the mixer properly positioned to
break up the ice and intimately mix the refrigerant with the reactor
contents.
79
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80
A cylindrical reactor was designed and built to replace the
original reactor. The cylindrical reactor was also constructed of
1/4-inch-thick Plexiglas. It was 5 inches in diameter and 11-1/2
inches tall. Four 1/2-inch diameter ports for temperature
measurement, vacuum measurement and maintenance, and nüscellaneous
other purposes were located along the sidewall. An integral diffuser
similar in construction to the diffuser in the rectangular reactor
was tooled in the base of the reactor. The channels formed a spiral
instead of a rectangular grid.
Another four ports, 1/4-inch in diameter, were located in the
reactor cover. Like the original reactor, the new reactor cover also
supported a mixer shaft bearing plate.
The reactor was modified several times during the course of
preliminary studies. Four 1/4-inch wide baffles running the height
of the reactor, equally spaced along the side wall, were added to
improve mixing. Modifications were also made to the mixer bearing to
accomodate a larger mixer.
Both reactors were originally equipped with integral diffusers.
However, these diffusers were prone to clogging. Distribution of
refrigerant was uneven, with most issuing from openings along the
wall of the reactor, promoting flash freezing at the wall. when the
original diffusers were found to be unsuitable, a number of different
diffuser types and configurations were tested. An aluminum base was
constructed with channels similar to those in the original reactor
base. Instead of entering the reactor through small holes, the
81
refrigerant flowed into the reactor through fine, spherical porous
diffusers. However, combined head loss through the channels and the
diffusers proved too great, causing liquid butane to vaporize before
emerging from the diffusers. Similarly, discs of finely divided
brass, set into the base, created too much head loss in the system.
Since the aluminum base was a large cold sink, it was ultimately
abandoned. The original reactor base was replaced by an unperforated
Plexiglas disc. Refrigerant was fed into the reactor through one of
the sidewall ports. 0n the inside of the reactor, a short length of
1/4—inch-diameter Tygon tubing connected the port fitting to a
pyramidal coarse bubble diffuser. This diffuser tended to ice,
especially at long detention times, and was replaced in later
experiments by a coil of I/4-inch copper tubing perforated with
0.012-inch holes.
Mechanical mixing was provided in all reported experiments to
promote intimate contact between sludge and refrigerant or hydrating
agent. In initial studies, a small laboratory mixer with a maximum
speed of I00 rpm was used. This proved insufficient to prevent the
formation of solid ice on the reactor surfaces, along the mixer shaft
and blades, and on the diffuser itself.
This mixer was eventually replaced with a Sears I3-inch,
5-speed, 3.0-hp drill press. The drill press not only unade high
speed mixing up to 2000 rpm possible, but also provided a stable‘
support for the reactor. However, while higher speeds reduced
diffuser icing significantly and prevented formation of solid ice
82
along the reactor walls and mixer shaft, they also resulted in
deterioration of sludge dewatering characteristics. A constant
mixing speed of 400 rpm was selected as a result of a series of
mixing tests on samples of RAAP alum sludge. At this speed, both the
negative effect on dewatering characteristics and the formation of
ice on surfaces were minimized.
Heat Exchange Systems
Heat exchange systems were necessary to maintain reactor and
refrigerant temperatures at optimum levels for butane and Freon
conditioning during experiments. Sludge samples were precooled to
minimize the use of refrigerant for this purpose. Systems for
temperature and vacuum/pressure maintenance and methods of sludge and
refrigerant precooling are discussed in the following subsections.
Temperature and Vacuum/Pressure Maintenance - To maintain
desired temperatures, the reactor was wrapped with uninsulated Tygon
tubing and encased by a two-inch-thick styrofoam jacket. Cooled
ethylene glycol was pumped from the well of a refrigerating bath
(Master Scientific Formaline Model 2095 Bath and Circulator) through
Rubatex-insulated tubing, around the reactor and back to the
reservoir of glycol.
Process temperature was maintained between -1 and +100 during
butane experiments. The temperature generally dropped over the
course of an experiment from the range of +0.5 to +100, to the range
of -0.5 to -100 as the sludge froze. A 4-cm Hg vacuum was
83
maintained in the reactor during butane experiments using a Gast air
compressor (Model DOA-P106-AA), piped to produce a vacuum. The
vacuum insured that the butane evaporated at operating temperatures.
For Freon 12 experiments, precooling the reactor in a commercial
refrigerator to 4 to 806 was sufficient to maintain the temperature
at desirable levels. Pressure—temperature conditions during Freon 12
experiments were maintained at points slightly below the vapor
saturation curve (Figure 6). (Hydrates form at all points beneath
this curve and above the gas hydrate formation curve at temperatures
less than 1206. However, reactions rates are more rapid at points
close to the vapor saturation curve.) Process temperature was
generally maintained between 7 and 1006; process pressure was varied
accordingly from 56 to 62 psia (3.9 to 4.3 x 105 Pa), using a Gast
Super Series air compressor (Model ROA-P101-AA). .
After conditioning, the temperature of the sludge was allowed to
rise above 1406 in order to decompose the hydrates. The pressure in
the reactor was subsequently increased to compress the Freon 12 to a
liquid state, as allowing it to bubble through the sludge resulted in
foaming. The liquid Freon floated to the surface and was then
allowed to evaporate.
Refrigerant Precooling - Butane was precooled to temperatures
ranging from -10 to -506 by feeding it through a 1/4-inch-diameter
copper coil (approximately two meters total length) submerged in a
bath of ethylene glycol and ice. Low temperatures were necessary to
prevent premature volatilization of butane due to heat gains in the
84
refrigerant feed system. Excessively low temperatures were avoided
to prevent exacerbating diffuser icing.
Freon 12 was precooled to 2-1/2 to 300 by immersing the copper
coil in ethylene glycol contained in the well of the refrigerating
bath.
Sludge Precooling - Samples of sludge were precooled before
introduction into the reactor. For butane experiments, two-liter
samples of sludge were precooled in a conventional commercial
deep-freeze unit for approximately four hours, until the sludge
temperature dropped to between +0.5 and +100. For Freon 12
experiments, samples were precooled to 4 to 800 in a commercial
refrigerator.
Refrigerant Feed Systems
Two types of refrigerant feed systems were utilized in
preliminary experiments: a conventional liquid system and a
polyaphron system. The polyaphron system was not used in later
experiments due to mechanical difficulties and foaming problems.
Both methods are discussed in the following subsections.
Conventional Liquid Systmn - Butane and Freon 12 were pumped
through the feed system using the compressive force of the
pressurized containers in which the refrigerants were purchased.
Butane pressure varied from 22 psi to 37 psi (1.5 to 2.6 x 105 Pa),
and Freon 12 pressure from 70 to 95 psi (4.8 to 6.6 x 105 Pa),
depending on room temperature. The tanks were tilted or turned
85
upsidedown, placing the feed valve below the bulk of the container
contents to insure that the refrigerant emerged from the cylinder as
a liquid.U
The feed system was constructed of 1/4-inch-diameter Polyflo
tubing, insulated with Rubatex. Liquid refrigerant flowed from the
tank through a precooling copper coil to a Gilmont rotameter for flow
measurement. Butane flow rate was adjusted with a union bonnet
metering valve. Freon 12 flow rate was adjusted with an ultra-fine
low-flow metering valve. A check valve in the line just prior to the
reactor prevented backflow of the reactor contents into the feed
line.
Butane flow rates between 5 and 35 mL/min were used in
preliminary experiments. Based on the results of these experiments,
a flow rate of 20 nm/min was selected for the remaining studies.
Higher flow rates resulted in flash freezing, while it proved
difficult to maintain a constant vacuum at lower flow rates.
Freon 12 flow rates between 5 and 25 mL/min were used in
preliminary experiments. A flow rate of 10 mL/min was selected for
the remaining studies. Higher flow rates resulted in an excessively
foamy product, while lower flow rates resulted in very long detention
times.
Polyaphron System — As an alternative method of introducing
butane into the sludge, experiments were conducted to incorporate
liquid butane into colloidal aphrons. Colloidal aphrons are finedroplets of water—insoluble gas or liquid, each encapsulated in a
86
thin surfactant film72. They exhibit unusual foam-like properties,
including great stability, and have been shown effective in
separation techniques73. Potential benefits in using liquid butane
in a polyaphron included storage and feeding at ambient pressure and
improved contact between butane and sludge.
The standard procedure used to produce aphrons is to add an oil
to a surfactant in solution. Initially one or two drops are added at
a time, with vigorous shaking between additions. Once a milky foam
begins to form, indicating the presence of aphrons, larger quantities
of oil are added.
The ultimate ratio of oil to water is approximately 10:1. Thus,
if 500 mL of oil aphrons are desired, 500 mL of the selected oil are
added to 50 mL of the surfactant solution.
Certain new techniques had ·u¤ be developed to produce butane
aphrons since liquid butane vaporizes at ambient temperature and
pressure. To maintain butane as a liquid at atmospheric pressure,
its temperature must be maintained below 000. Glycerol must be added
to the surfactant solution to prevent it from freezing during
production and storage.
The procedure developed was as follows:
1. Three to four gallons of ethylene glycol were chilled to
-2000. A plastic container and a dropper bottle were also·
chilled. The plastic container was weighted so that itcould not float when submerged in the glycol.
87
2. Two coolers were prepared to hold the glycol. One gallon
of the chilled glycol was poured into one cooler, and the
rest into the second cooler.
3. A solution of 5 g/L sodium dodecyl benzene sulfonate (SDBS)
was prepared. To make 250 mL of oil aphrons, 25 mL of 5
g/L SDBS, 10 mL of glycerol, and 2.5 mg of lauric acid were
added to the plastic container. Solution temperature was
allowed to decrease to -1OOC in the larger cooler.
4. Liquid butane was fed into the dropper bottle until it was
three-quarters full. The dropper bottle was then attached
to the side of the cooler that contained the gallon of
glycol, with the bottle immersed in the glycol.
5. The butane was added to the surfactant solution with the
dropper one drop at a time, with vigorous shaking
maintained for about one minute between drops. After five
drops were added in this manner, two to three drops could
be added at a time. The amount of butane added was
gradually increased to 5 mL. However, this much was not
added until the solution had a thick, milky appearance.
Adding too much butane too soon caused the aphrons to
destabilize and fall apart.
88
6. Once formed, the aphrons were stored in a commercial
deep-freeze unit.
It was discovered that too low a storage temperature caused the
surfactant solution to freeze and settle to the bottom, leaving the
liquid butane floating at the surface. If the solution was
vigorously shaken and warmed so that the solution thawed, the aphrons
reformed, as long as the temperature did not rise above OOC.
Based on this discovery, a new method was devised to produce the
aphrons. The surfactant solution, glycerol, and lauric acid were
added to a plastic container. Butane was added gradually as
described above until four to five drops of butane were added at a
time, with vigorous shaking between additions. The solution was then
put in a freezer and the surfactant solution allowed to freeze. The
aphrons reformed after five to ten minutes of vigorous shaking.
Relatively large amounts of butane (up to 1O mL per addition) were _
then added to produce the desired quantity of aphrons.
The butane aphrons proved difficult to pump. Contact with the
pump and tubing, which could not be maintained satisfactorily below
OOC, caused the aphrons to volatilize prematurely. Similar problems
with premature volatilization were encountered with gravity feed.
Conditioning Agent Removal
Various techniques were used during the early stages of this
study in an attempt to remove spent butane and Freon 12 from the
89
product sludge. Neither vacuum stripping nor aeration resulted in
any observable improvement in dewatering characteristics for either
butane- or Freon—conditioned sludges.
Overnight storage at 40OF, on the other hand, improved the
dewatering characteristics of both butane- and Freon-conditioned
sludges. Product sludges, which in general exhibited very poor
settling characteristics immediately after thawing, usually separated
into sludge and supernatant fractions with storage. Certain
butane-conditioned samples produced a third fraction, a stable,
high-solids foam with poor dewatering characteristics.
ANALYTICAL METHODS
Table 7 lists analyses and determinations used to quantify the
results of conditioning experiments. Descriptions of analytical
methods are presented in this section.
Particle Size Distribution
Particle size distributions of sludge and supernatant samples
were analyzed to gauge any changes which occurred during conditioning
which might impact dewatering characteristics. Particle counts were
made using a HIAC Particle Size Analyzer Model PC-32074. The sensor
used in this study was a HIAC Standard Sensor Model CMB-300, which is
capable of detecting and counting particles in the range of 5 to 300
microns (um).
90
TABLE 7I
EXPERIMENTAL ANALYSES AND DETERMINATIONS
Analysis/Determination Reference
Total Particle Counts 74
Particle Size Distributions 74
Weight Fractions 75
Specific Resistance 6
Blinding Index 9
Vacuum-Filtered Cake Solids Concentration 75
Initial Solids Concentration 75
Centrifuged Solids Concentration 75
Floc Density 76
Supernatant TOC 75
Sludge pH 75
91
Samples were diluted, if required, to meet the particle
concentration limit of the sensor. If available, filtered
supernatant was used to dilute samples. If not, tap water was used
for dilution. Usually sludge samples were diluted to 1/1000, and
supernatant to 1/10, if at all. Three 10-mL aliquots of each sample
were analyzed for particle size distribution, and the results of the
three averaged.
Results are reported as totals per "mean particle diameter
(MPD)." MPD was calculated by averaging the end points of each size
range (e.g., if the particle sensor limits for a given range were set
at 35 and 45 um, the MPD is 40 um.) (This nomenclature is not
intended to imply that particles are spherical or that the
measurement reported is a characteristic length as determined by
Knocke and wakelandlo. Rather it is a convenient term to describe
the dimension of the particle sensed by the analyzer.)
Prior to analysis, samples were filtered through a brass screen
(250 um pore openings) to prevent clogging of the sensor. A sample
of the filtrate was weighed before and after drying at 103OC and the
percentage of solids passing through the filter determined (in
accordance with Section 209A of Standard Methods75. This calculated
value was reported as percent of sludge solids passing a 250-um
sieve.
92
Specific Resistance, Initial and Vacuum-filtered Solids
Concentrations, and Blinding Coefficients
Specific resistance was calculated using the results of time vs.
volume data obtained using Grade 40 filter paper (8 um particle
retention) in a Buchner funnel apparatus as described in Vesilindö.
A vacuum of 20 in Hg (508 mm Hg) was drawn on the filtering apparatus
during the procedure. At cake failure, a sample of the sludge cake
was scraped from the filter, and the dry solids concentration
determined according to procedures described in Section 209A of
Standard Methods75. If no cake was produced within 30 minutes, a
representative cake solids concentration was used to calculate
specific resistance. Generally, this value was that determined for
the cake produced at the lowest conditioning dose for which a cake
formed. Initial dry solids concentration was determined according to
the same procedure.
The blinding coefficient, as defined by Huangg, was determined
by plotting the natural logarithm of the time and volume data from
the Buchner funnel test and calculating the slope of the resultant
line.
Centrifuged Solids Concentration
Samples of sludge were distributed equally between 2 plastic
50-mL test tubes and placed in a Beckman Model J-2IC centrifuge.
Samples were centrifuged at 9000 rpm for ten minutes. Supernatant was
then decanted, the solids removed from the tube, and the dry solids
93
concentration of the resultant cake determined by drying at 1030075.
Floc Density
The floc density of selected sludge samples was measured to
determine if conditioning had any effect on the relative water
content of flocs. Density was analyzed using the method described by
Vollrath-Vaughn76. Small droplets of sludge were introduced beneath
the surface of stratified layers of various concentrations of Percoll
contained in a 10-mL test tube. (Percoll is a polymer-coated silica
sol manufactured by Pharmacia Fine Chemicals, which can be
concentrated to specific gravities of up to 1.3.) The test tubes were
centrifuged in an International Clinical Centrifuge Model CL at 850
RPM for two minutes. Upon removal, the samples were observed and the
location of flocs noted. Flocs tended to concentrate either within a
particular gradient step or between two adjoining gradient steps.
Commonly, particles concentrated in bands at several locations,
indicating a range of densities. The samples were returned to the
centrifuge for another two minutes and then removed. Location of
floc bands was again noted.
Total Organic Carbon
The total organic carbon (TOC) content of supernatant samples
was measured to assess the (effect of conditioning on supernatant
quality. TOC was analyzed using a Horiba Total Organic Carbon
Analyzer Model PIR-2000. This analyzer utilizes the
94
persulfate-ultraviolet oxidation method described in Section 505A of
Standard Methods75.
Sludge pH
The pH of sludge sampies was measured using a Fischer Scientific
Accumet pH meter Model 610, according to the procedure described in
Section 423 of Standard Methods75.
95
IV. RESULTSl
The results of direct-contact, freeze-thaw conditioning
experiments are presented together with the results of polymer and
indirect—contact experiments in this chapter. Each of the following
sections is devoted to a specific sludge.
STROUBLES CREEK WASTE ACTIVATED SLUDGE
Samples of unconditioned waste activated sludge obtained from
the Stroubles Creek Wastewater Treatment Plant dewatered rapidly to a
moderate solids concentration. As the specific resistance of the
sludge was already low prior to conditioning, the main benefit
anticipated from conditioning was an increase in dewatered solids
concentration.
Polymer conditioning typically increases filtration rates while
having little effect on final dewatered solids concentrations.
Freeze—thaw conditioning, in contrast, was expected to produce
significant increases in solid concentration. Certain improvements
in filtration rates were also anticipated.
Polymer Conditioning
Samples of Stroubles Creek waste activated sludge were
conditioned with 10, 20, 30 and 50 mg/L Betz 1160. There was little
96
change in dewatering characteristics for any polymer dose. The
primary conditioning effect of polymer addition was an increase in
sludge floc size. The limited improvements observed when polymer was
added to this particular sludge suggested that an increase in floc
size does not automatically result in significant improvements in
sludge dewatering characteristics.
The results of analyses and determinations on
polymer-conditioned samples of waste activated sludge are presented
in Table 8.
Particle and Chemical Characteristics - The main effect of
polymer conditioning on waste activated sludge was a shift in
particle size distribution to size ranges with larger mean particle
diameter (MPO). As can be seen from Figure 8, conditioning reduced
the total number of particles with MPD less than 55 pm, especially in
the size ranges with MPD less than 30 pm. Reduction in the
percentage of small particles varied consistently with polymer dose.
The greatest reduction was achieved at the highest polymer dose: the
number of particles with MP0 less than 55 tun was reduced froni 95
percent for the unconditioned sample to 84 percent for the sample
conditioned with 50 mg/L polymer. Also, 10 percent of the particles
in this sample were retained when filtered through a 250-pm sieve,
compared to no measurable percentage for all other samples. These
results indicate a substantial shift towards larger sizes in the4
distribution of particles.Polymer conditioning had little effect on the supernatant, other
97
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FIGURE 8. PRRTICLE SIZE DISTRIBUTIONS. POLYMER-CONDITIONED WRSTE HCTIVFITE0 SLUDGE.
99
than slightly reducing the total number of particles with MP0 less
than 250 um.
Dewatering Characteristics - The overall effect of polymer
conditioning on the dewatering characteristics of waste activated
sludge was minimal. The dewatered solids concentration obtained from
both vacuum filtration and centrifugation decreased slightly for all
conditioned samples. Contrary to expectations, specific resistance
did not decrease with increasing polymer dose or with increases in
particle size, showing instead only slight variations from the value
calculated for the unconditioned sludge. All calculated specific
resistance values were less than 100 x 10ll m/kg.‘ The altered appearance of sludge flocs observed during floc
density analyses suggested that; the decreases in dewatered solids
concentration resulted from retention of previously free water within
the polymer-enhanced floc structure. when polymer was added to the
sludge, formerly fine, isolated flocs aggregated together into large,
amorphous clumps. As small amounts of free water were incorporated
into the growing aggregates, the amount of moisture available for
extraction by dewatering was reduced, resulting in decreased
dewatered solids concentration.
Other parameters were unaffected by the restructuring of
particle groups. Free water still drained through the new structures
at similar rates, as measured by the specific resistance, and changes
in the amount of water associated with the particle were not
sufficient to affect floc density.
T 100
Changes in blinding coefficient supported the indications of
increased sludge floc size observed in particle size data. Three of
the four conditioned sludges had negative blinding coefficients in
contrast to the unconditioned sludge, which had a blinding
coefficient of zero. The decrease in this parameter may have
resulted from an increasing homogeneity in particle size, as
particles were bound together by polymer, as suggested by Notebaert5.
Indirect Contact, Freeze-Thaw Conditioning
The major effects of indirect-contact, freeze-thaw conditioning
of Stroubles Creek waste activated sludge on parameters of interest
were large increases in initial and vacuum-filtered solids
concentration and hi floc density. These changes signalled major
alterations in floc structure and substantial decreases in floc water
content. There were also moderate increases in specific resistance,
most likely related to increases in solids content.
Results of these and other analyses and determinations on the
sample of indirect-contact, freeze—thaw conditioned waste activated
sludge are presented in Table 9.
Experimental Observations — Certain distinct changes in the
appearance and gross settling characteristics of indirectly frozen
waste activated sludge were observed. After thawing, the conditioned
sludge settled rapidly, and a large volume of supernatant was
decanted easily. The freeze-thaw solids were large, grainy, and
dense, similar in appearance to freeze—dried coffee granules.
‘ 101
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Particle and Chemical Characteristics - The overwhelming
difference between the particle distributions of indirect-contact,
freeze-thaw conditioned and unconditioned samples of waste activated
sludge, depicted in Figure 9, was in the total number of particles
represented by the distributions. The conditioned sludge sample had
20 percent fewer particles with MP0 less than 250 um. Similar
reductions in the number of particles in the supernatant with MPD
less than 250 pm were noted.
The small particles eliminated by conditioning from the
distributions measured by the particle counts constituted part of the
mass of larger particles retained on a 250-um sieve. Particles with
MPD greater than 250 um represented 76 percent by weight of the total
solids of the conditioned sludge sample, compared to the
unconditioned sample, which had no measurable percentage in that size
range.
Changes iri waste activated sludge ini with freezing indicated
that physical disruption of particles during freezing may have
occurred. Sludge pH increased from 7.0 for the unconditioned sample
to 9.3 for the conditioned sample. Chemically neutral particles
might have broken apart during freezing to release alkaline
components into the supernatant, causing the sludge pH to increase.
Indirect freezing resulted in a large increase in floc density,
from 1.03 to 1.05 g/L. The increase in density was readily apparent
from the greatly improved settling characteristics of the freeze-thaw
solids, as well as the appearance of individual particles. Mass
103
3000
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FIGURE 5. PFIRTICLE SIZE DISTRIBUTIONS. INDIRECT-CONTRCTFREEZESTHFIU CONDITIONED HRSTE HCTIVFITE0 SLUDGE.
104
balance calculations showed that this represented the release of 53
percent of the floc water.
Dewatering Characteristics - Indirect-contact, freeze-thaw
conditioning of waste activated sludge resulted in a large increase
in initial and vacuum-filtered dry solids concentration and moderate
increases in specific resistance. The process released a large
amount of water as supernatant, increasing the initial solids
concentration of the sludge over 300 percent. Vacuum-filtered solids
increased by 51 percent, and centrifuged solids posted a smaller but
still sizable increase of 15 percent.
The concomitant increases in dewatered solids concentration and
floc density were probably related. Arundel77, in her study of the
dewatering behavior of sludges exposed to high pressures, observed
increases in floc density with increased dry solids above a
sludge-specific concentration. She concluded that internal water was
released from the flocs, causing floc density to increase, as
pressure deformed the floc matrix. The intense pressures developed
during freezing have been suggested as possible causes of similar
results by other researchers63’78.
Specific resistance more than doubled with indirect freezing,
although the value calculated for the conditioned sample was still
moderate (120 x 1011 m/kg). Increased solids content has been shown
to increase specific resistancea, and it is likely that the large
change induced by freezing in initial solids affected the sludge's
response to filtration.
105
The change in blinding coefficient with indirect-contact
freeze-thaw conditioning suggested that conditioning enhanced the
tendency of the sludge cake to blind,. The blinding coefficient
increased from zero for the unconditioned sludge to a positive value
for the conditioned sludge. The usual interpretation of a positive
blinding coefficient---the blocking of cake pores by small
particles---was not suggested by particle size analysis data, which
showed a definite increase in particle size. Considered with the
increased specific resistance, the positive blinding coefficient may
have indicated changes in cake structure. Under vacuum, larger flocs
may have compressed, resulting in a more tightly packed cake less
conducive to drainage.
Direct-Contact, Freeze—Thaw Conditioning with Butane
One-L samples of Stroubles Creek waste activated sludge were
conditioned with 20 mL/min butane for contact times of 20, 30, and 40
minutes, for total butane doses of 400, 500 and 800 mL/L,
respectively. Direct-contact freeze-thaw conditioning <yf Stroubles
Creek waste activated sludge with butane produced no significant
improvements in dewatering characteristics. 0nly small increases in
centrifuged solids were observed. Changes in vacuum-filtered solids
were variable, and specific resistance increased for all butane
doses.
Indirect freezing of waste activated sludge also resulted in
increased centrifuged solids and increased specific resistance.
106
Evaluation of particle size distributions suggested, however, that
different mechanisms were responsible for similar results.
Analyses were performed on unconditioned and conditioned samples
of waste activated sludge conditioned with butane to determine
particle and dewatering characteristics. Results of analyses and
determinations are presented in Table 10.
Experimental Observations — Conditioning produced a foamy,
poorly settling product sludge. The foam, high in solids content and
difficult to dewater, was stable, dissipating only slightly with
gentle mixing.
Particle and Chemical Characteristics - The main result of
direct-contact, freeze-thaw conditioning of' waste activated sludge
with butane was an increase in the number of small particles in the
product sludge. The changes in particle size distribution were not
likely caused by the conditioning mechanisms of the freeze-thaw
process alone, however, but influenced by other factors.
The particle size distribution for the sludge conditioned with
400 mL/L butane, shown in Figure 10, is representative. The
distribution of the conditioned sludge sample, similar in shape and
magnitude to that xyf the unconditioned sample, comprised a nmch
larger number of particles in size ranges with mean particle diameter
(MPO) less than 25 pm. The total number of sludge particles with MPD
less than 250 pm nearly doubled for the 600 mL/L and 800 mL/L butanel
doses.
Conditioned supernatant samples also had more small particles
107
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MEHN PRRTICLE DIGMETERH MICRONS
FIGURE 10. PRRTICLE SIZE DISTRIBUTIONS. WRSTE RCTIVHTEDSLUDGE CONOITIONED WITH 100 ¤•L1L BUTFINE.
109
than unconditioned supernatant samples. The particle size
distribution of the conditioned samples comprised a. much greater
number of particles in size ranges with MPD less than 30 pm, and
exceeded the unconditioned distribution in all size ranges with MPD
less than 50 um-
The changes observed in the particle size distributions of
conditioned samples may have been caused by (1) the reduction of
particle size during freezing, either through compression or
disruption; and/or (2) floc shear induced by mixing applied during
experiments. Compression of particles was not substantiated by floc
density measurements, which did not change with conditioning.
Certain evidence of particle disruption was observed in the results
of indirect freezing of waste activated sludge, although the particle
size data from those experiments seemed to indicate that these
fractionated particles reaggregated upon thawing. If the butane
conditioning experiment likewise resulted in particle disruption, it
is possible that reaggregation was prevented by the foam generated
during the experiment. Mixing could also have contributed to reduced
particle size through floc shear or by preventing smaller particles
created by freezing from reaggregating. (Mixing tests of equal
intensity and duration conducted in the experimental apparatus used
in this study produced similar changes in particle size
distributions.)
Increases in supernatant TOC were noted for all conditioned
samples. The increases for the samples conditioned with 600 mL/L
110
butane were moderate, while the increase for the sample conditioned
with 400 mL/L was excessively large. Moderate increases in TOC
concentration might be attributed to any of several causes, including
the release of organics as particles ruptured during freezing, the
suspension of fines in the supernatant as a result of mixing, or
entrainment of butane. The large TOC increase observed at the lowest
butane dose was likely due to the entrainment of excessive amounts of
butane in the sludge during this experiment, which generated large
amounts of foam.
Dewatering Characteristics - There was no overall improvement in
the dewatering characteristics of butane-conditioned waste activated
sludge. while centrifuged solids increased slightly for all butane
doses, the response to vacuum filtration was poor. Specific
resistance increased for all butane doses, Final vacuum-filtered
cake solids increased only slightly with the application of 400 mL/L
butane and decreased with the application of 600 mL/L and 800 mL/L
butane.
The deterioration of specific resistance with conditioning is
shown in Figure 11. The increase in specific resistance in the
indirect·contact, freeze-thaw experiment was attributed to the
increased solids content, which resulted from the release of internal
water. Thus the change in specific resistance for indirectly frozen
sludge, though undesirable, was assumed to be part of the
conditioning effect of the freeze-thaw process.
111
300I.! ··
3CJ•-•x
.3*; 200LJLJZCEI-(0•—•(0La.!0:LJ•-•LL 100•-•LJIJJO.(0
Ü
0 0 200 400 600 800 1 000BUTHNE DOSE. ••L/L
FIGURE 11.. SPECIFIC RESISTFINCE V5 BUTRNE DOSE.BUTRNE-CONDITIONED VRSTE RCTIVFITED SLUOGE.
112
In contrast, changes in particle size distribution in the
direct-contact, freeze-thaw experiments suggested that the increase
in specific resistance for butane-conditioned sludge was related to
process variables independent of. or extraneous to the actual
conditioning process, i.e., mixing and foaming.
In considering the causes of the increases in specific
resistance, it is interesting to note that higher butane doses
resulted in relatively lower specific resistances. In addition, a
positive blinding coefficient was calculated for the sludge treated
with 400 mL/L butane, in contrast to the other samples, conditioned
and unconditioned, which showed no evidence of cake blinding. Since
higher butane doses were administered over longer contact times, and
thus longer mixing times, specific resistance would be expected to
increase with butane dose if deterioration was due to mixing alone.
The decrease observed in specific resistance with high butane dose
suggests that (1) deterioration of dewatering characteristics was not
caused by mixing alone, but by some other factor as well; and (2)
higher butane doses and/or longer mixing times mitigated the negative
effect of this other factor.
Certain observations suggest that the foam generated during the
process was the factor. First, the foam, produced whether mixing was
provided or not, tended to dissipate at longer mixing times.
Therefore, foam would be more likely to affect specific resistance at
shorter contact times. Second, the characteristics of foam make it a
likely cause of poor dewatering.
113
The changes in vacuum-filtered solids---an increase at 400 mL/L
butane and decreases at 600 mL/L and 800 mL/L butane---suggested that
the extent to which conditioned sludge dewatered upon vacuum
filtration depended less upon the foam content of the sludge than did
filtration rate. The variability in size and direction of these
changes precludes any conclusions as to their meaning.
The slight increase in centrifuged solids probably resulted from
the separation of previously bound water from sludge solids as flocs
were broken apart by freezing pressures or by inixing turbulence.
Certain factors, such as altered particle size distributions and the
flow—inhibiting characteristics of the foam, which prevented the
removal of this water by vacuum filtration, did not affect its
removal by centrifugation, which tends to enhance foam drainage. ·
In summary, butane conditioning of waste activated sludge
resulted in a poorly dewatering product. The effects of mixing and
of foaming were severe enough to counteract any beneficial effect of
the freeze—thaw process. Longer conditioning times resulted in less
deterioration of specific resistance values, but no overall
improvement in dewatering characteristics.
Results were disappointing when compared to the increases in
vacuum-filtered solids obtained with indirect freezing, but it must
be recalled that neither polymer conditioning nor indirect freezing
improved specific resistance, and that polymer conditioning actually
resulted in small decreases in the vacuum-filtered cake solids
concentration.
114
Direct-Contact, Freeze-Thaw Conditioning with Freon 12
0ne-L samples of Stroubles Creek waste activated sludge were
conditioned with Freon in batch and continuous experiments. In the
batch experiments, samples were treated in one- and two-stage
conditioning, with 250 mL Freon applied at each stage. In the
continuous experiments, samples were fed 10 mL/min Freon for contact
times of 25, 50, and 75 minutes. Thus the samples treated in
one-stage batch and 25-min continuous experiments were fed 250 mL/L
Freon; the two-stage batch- and 50-min continuously conditioned
samples, 500 mL/L; and the three-stage batch- and 75-min continuously
conditioned samples, 750 unL/L. It should be noted as well thatC batch-conditioned samples were mixed for very short periods at the
beginning of each experiment to insure intimate contact with the
refrigerant, while continuously conditioned samples were mixed
throughout the defined contact time.
The effects of direct-contact, freeze-thaw conditioning of
Stroubles Creek waste activated sludge with Freon 12 on dewatering
characteristics were varied. Conditioning resulted in large
increases in vacuum-filtered solids and smaller, but still sizable,
increases in centrifuged solids. Increases in specific resistance
were very large. Changes in particle distributions were not
straightforward, and were likely influenced by handling
inconsistencies.
Although increases in solids concentration were similar to those
obtained in indirect freezing, changes in particle characteristics
115
for Freon-conditioned samples suggested that mixing and foaming
effects interfered with the rate of dewatering.
The results of analyses and determinations from batch and
continuous experiments on Freon-conditioned samples of waste
activated sludge are presented in Tables 11 and 12, respectively.
Experimental Observations - The Freon-conditioning process
resulted in a foamy product sludge; the foam, however, was not
produced in the large quantities noted in the butane-conditioning
experiments, nor was it stable, tending to disperse with overnight
storage.
Particle and Chemical Characteristics - Unlike the changes
noted as a result of polymer addition, indirect freezing, and direct
freezing with butane, changes in particle size distributions for
Freon-conditioned waste activated sludge samples followed no distinct
trend.
In general, particle size distributions for both batch- and
continuously conditioned samples were very similar in shape and
magnitude to those of unconditioned samples, as can be seen from
Figures 12 and 13. All continuously conditioned samples had a
greater number of particles with mean particle diameter (MPO) of 10
pm, suggesting that, as for butane conditioning, there was some
mixing-induced floc shearing.
The total number of particles with MPD of 250 pm or less in
Freon-conditioned samples generally decreased, however, in contrast
to the sizable increases observed in butane-conditioned samples.
116
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FIGURE 12. PRRTICLE SIZE DISTRIBUTIONS. FREONCONDITIONEDHFISTE FICTIVFITED SLUDGE (BHTCH EXPERIMENTS1
119
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FIGURE 13. PFIRTICLE SIZE DISTRIBUTIONS. FREON.CONDITIONED UFISTEI HCTIVFITED SLUDGEKCONTINUOUS EXPERIMENTS 1
120
This suggests that there may have been an increase in the number of
particles with MPD between 55 and 250 um. (There was no measurable
solids fraction with MPD greater than 250 pm.)
Batch-conditioned supernatant samples had a very large total
number‘ of particles, up to seven times that <rf the unconditioned
samples. Most continuously conditioned samples also had large
numbers of particles in the supernatant.
Supernatant particle size distributions had two distinct shapes.
The first decreased steadily, at a decreasing rate, as particle size
increased, and was similar to distributions observed in other
experiments for both conditioned and unconditioned samples. The
second was relatively flat for size ranges with MPD less than 35 um,
and then decreased in a similar manner to the first distribution.
Each of the two distributions were observed for both conditioned and
unconditioned samples, and the second was characteristic of
supernatant which has been allowed to settle, suggesting that these
differences were the result of unintentional inconsistencies in
sample preparation prior to particle analysis.
J There were small decreases in floc density noted for both batch
and continuously conditioned samples. These decreases would imply
the association of previously unbound water with sludge flocs, if
that conclusion were not contradicted by the increase in dewatered
solids concentrations discussed below. Given the increase in
dewatered solids, it is more likely that any decrease in floc density
resulted from the association of Freon bubbles with the flocs, giving
121
rise to the foam observed in all samples.
TOC increased moderately with conditioning, from values of 8 to
12 mg/L for unconditioned samples, to values of 34 to 54 mg/L for
conditioned samples. TOC tended to increase with increasing total
Freon volume applied. TOC had also increased for butane-conditioned
samples, and it was speculated that the source of a certain fraction
of the TOC was entrained butane. Unlike butane, however, Freon is
not measured by TOC analyses. The increase in organic carbon must
have originated from a different source, either from particles
ruptured during freezing or as fines produced by mixing.
Dewatering Characteristics - There were increases in
vacuum-filtered and centrifuged solids respectively for certain
batch- and continuously Freon-conditioned samples of waste activated
sludge. Vacuum-filtered solids increased 63 percent for one-stage
conditioning, approaching the level of improvement established by
indirect conditioning. Continuous conditioning with 250 and 500 mL/L
Freon resulted in smaller increases. In contrast, the sample
conditioned with 750 mL/L Freon produced no cake at all in 30 minutes
of dewatering.
Centrifuged solids concentration increased by percentages
similar to that obtained with indirect freezing. Smaller increases
were obtained with higher doses, whether administered continuously or
in stages. Improvement in dewatered solids for indirectly frozenO
sludge was attributed to the removal of floc moisture. As water was
squeezed from the floc, the floc became more compact and, thus, more
122
dense. According the the alternative interpretation, particle
structuress were broken apart, releasing water, and then recoalesced
in new floc structures of higher density. In either case, increases
in dewatered solids were accompanied by increases in floc density.
As suggested above, the decrease in floc density observed in
Freon-conditioned samples was likely the result of the foam formed by
the Freon bubbling through the sludge during the freeze-thaw process.
The conditioning effect of the Freon might have resulted in net
increases in density, had the conditioning process not been
compromised by the effects of foaming.
As can be seen from Figure 14, Freon conditioning of waste
activated sludge resulted in large increases in specific resistance,
which varied directly with Freon dose. Increases were very large for
Freon doses of 500 mL/L or more. The order-of-magnitude increases in
specific resistance, which worsened with higher Freon dose for both
batch- and continuously conditioned samples, were not likely the
results of changes in particle size distributions, which were
minimal, but more likely caused by the inclusion of Freon bubbles in
the sludge as foam. The increase was greatest for the two-stage
batch-conditioned sample, mixed only intermttently, than for the
continuously conditioned sample also treated with 500 mL/L, mixed
throughout the contact time. This is consistent with the
interpretation of the interplay of mixing and foaming developed in
the results of butane conditioning of waste activated sludge reported
in the preceding section; that is, longer mixing times ameliorated
123
3000Il
E ·••-«x2*; 2000uiI.)ZCE1-(D•-4(DLuII1-* 0•-•U- 1000•-«UuJO.LD E] BQTCHg CJ CONTINUOU6
00 200 400 600 600
FREON 005E. ¤L/L
FIGURE 11. SPECIFIC RESISTFINCE VS FREON DOSE.FREONCONDITIONED URSTE RCTIVRTE0 SLUDGE.
124 _
the negative effects of foaming.
STROUBLES CREEK PRIMARY SEWAGE SLUDGE
Samples of unconditioned primary sewage sludge from Stroubles
Creek wastewater Treatment Plant dewatered poorly. Not only did the
sludge filter very slowly, with high specific resistance, but no cake
formed during the Buchner funnel test. Conditioning was expected to
improve filtration rates and cake quality.
Polymer Conditioning
Samples of dry solids Stroubles Creek primary sewage sludge werel conditioned with 10, 20, 75, 100, 150, and 200 mg/L Betz 1160.
Polymer conditioning was successful in greatly decreasing specific
resistance, as well as producing a cake of moderate solids
concentration upon vacuum filtration at higher polymer doses. The
results of analyses and determinations on conditioned and
unconditioned samples of primary sewage sludge are presented in Table
13.
Particle and Chemical Characteristics - Polymer conditioning of
Stroubles Creek primary sewage sludge resulted in reductions of the
total number of particles with mean particle diameter (MPD) less than
250 um, as determined by particle counts, and in decreases in the
relative number of very small particles (MPD = 10 um).
As can be seen from Table 13, there was a steady decrease with
125
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increasing polymer dose in the total number of particles represented
by the particle distributions of sludge samples. There were only
slight changes in the weight fraction of total solids retained on a
250-um sieve in samples conditioned with less than 100 mg/L polymer;
however, samples conditioned with 100 mg/L or more showed large gains
in this fraction. Successively greater doses of polymer resulted in
fewer numbers of particles in each analyzed size range, especially in
size ranges with MPD less than 25 pm, as can be seen from Figure 15.
Like sludge samples, conditioned supernatant samples had many
fewer particles than the unconditioned supernatant sample, especially
in the size range with MPD equal to 10 um. The total number of
particles with MPD less than 250 um in most conditioned supernatant
samples did not decrease strictly with increasing polymer dose,
however. Anomalies may have resulted from handling inconsistencies
prior to settling. Large reductions in the number of small
particles (MPD less than 20 pm) in the supernatant at all polymer
doses were noted.
Floc density cM’ the primary sewage solids increased slightly
with polymer conditioning, with the bulk of particles increasing in
density from 1.05 and 1.06 g/L for the unconditioned sample and
samples conditioned with 100 mg/L polymer or less, to 1.07 g/L for
samples conditioned with 150 and 200 mg/L polymer.
Dewatering Characteristics - Dewatering characteristics of
Stroubles Creek primary sewage sludge improved greatly with polymer
conditioning. Specific resistance decreased for all polymer doses,
128
24UUÜ
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D.LL SUPERNFITFINTO 0EJ 6000 ~mE \¤Z _.
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LLO 1 S2 ggg ZÜÜÜ $2Lu — .. $1
. — 9 = _E 00 10 20 30 40 50 60HEQN PRRTICLE DIQMETER. MICRÜNS
FIGURE 15. PRRTICLE SIZE DISTRIBUTIONS. POLYMER-CONDITIONED PRIMRRY SEUFIGE SLUDGE.
129
as shown in Figure 16. Also, higher polymer doses succeeded in
producing a vacuum-filtered cake of moderate solids content, and
specific resistance was much reduced. It was likely that the
increasing improvement in dewatering characteristics of primary
sewage sludge conditioned with increasing amounts of polymer resulted
from the changes in particle size distribution; specifically, the
reduction in the number of small particles in sludge and supernatant.
Small particles are generally responsible for cake blinding, and
their presence and interference in the unconditioned sample was
signalled by a positive blinding coefficient.
The reversal of the sign of the blinding coefficient for all
conditioned samples as well as the ability of samples conditioned
with higher polymer doses to form a cake during vacuum filtration
probably resulted from an increase in the size of the particles
constituting the sludge.
Centrifuged solids, dewatered by different mechanisms and less
susceptible to changes in particle size distribution, remained stable
for all polymer doses. Had changes in floc density been associated
with changes hi the water balance, centrifuged solids might have
varied accordingly.
Indirect-Contact, Freeze-Thaw Conditioning
Indirect-contact, freeze-thaw conditioning of Stroubles Creek
primary sewage sludge resulted in a substantial decrease in specific
resistance. Although initial solids concentration more than doubled,
130
8000
äQ"° 6000xE"x¤uiLJZEan 4000•-•U')I.n.|C!LJI-OLL•-•L'] 2000D.U]
00 25 50 75 100 125 150 175 200POLYMER DOSE. ng/L
FIGURE 1B.” SPECIFIC RESISTFINCE VS POLYMER DOSE.POLYMER-CONDITIONED PRIMRRY SEUFIGE SLUDGE.
131
and particle characteristics showed a shift towards larger, more
dense particles, cake solids concentrations showed no improvement.
In general, indirect freezing was not as effective as polymer
addition in improving the dewatering characteristics of primary
sludge.Results of analyses and determinations for an indirectly frozen
sample and an unconditioned sample of Stroubles Creek primary sewage
sludge are presented in Table 14.
Particle and Chemical Characteristics - Indirect-contact, freeze
thaw conditioning of primary sewage sludge resulted in reduction of
the total number of particles represented by the particle size
distribution and in a decrease of the relative number of very small
particles (mean particle diameter (MPO) = 10 um). As can be seen
from Table 14, the total number of particles represented by the
distribution decreased sharply with conditioning, as did the weight
fraction of total solids passing through a 250-um sieve. As can be
seen from Figure 17, there were many less particles with MP0 equal to
10 mn in the conditioned sludge and supernatant samples, with the
conditioned samples also having fewer particles than the
unconditioned samples in each size range.
Average floc density of indirectly frozen primary sewage sludge
increased from 1.045 to 1.06 g/mL. The range of densities broadened,
with the lower limit extended from 1.055 to 1.03 g/mL, and the upper(
limit from 1.10 to 1.11 g/mL.
The changes in floc density suggested that the increase in
132
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Ü 20000QäZ 0 E __
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u3 6000ü' 6Lu06Ep-4 Ü
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HEGN PQRTICLE DIHHETEFL MICRONS
FIGURE 17. PRRTICLE SIZE DISTRIBUTIONS. INDIRECT-CONTRCTFREEZE-THFW CONDITIONED PRIMRRY SEHRGE SLUDGE.
134
particle size was not a simple amalgamation of existing flocs, as
occurred during polymer conditioning. Particle size changes were
more likely caused by destruction of existing floc structures during
freezing, resulting in the freeing of previously bound water, and
ensuing consolidation of released particles during thawing and
storage. This interpretation would explain the change in the range
of floc densities, which increased to encompass both less and more
dense flocs, created as old particle attachments were broken and new
ones formed, and the general increase in floc density, resulting from
the release of floc water.
Dewatering Characteristics — Indirect-contact, freeze-thaw
conditioning had varying effects on the dewatering characteristics of
Stroubles Creek primary sewage sludge. Initial dry solids
concentration increased over 100 percent, from 2.1 to 4.8 percent
solids, with indirect freezing, Neither the conditioned nor the
unconditioned sample, however, produced a cake after 30 minutes of
dewatering. Centrifuged solids actually decreased over 30 percent
with conditioning, from 17 to 11 percent solids.
There was a substantial decrease in specific resistance for the
conditioned sludge. As for the polymer-conditioned sludge, the
decrease was related to the increase in particle size. The decrease
was not, however, as large as that obtained by the higher doses of
polymer in comparative experiments. Changes in floc structure would
account for the decrease in specific resistance and the increase in
initial solids content. Likewise, the change in the blinding
135
coefficient from negative to positive could result from a more
tightly packed, and hence more compressible, cake structure,
facilitated by flocrestructuring.Direct-Cor
act, Freeze-Thaw Conditioning with Butane
A 1-L sample of Stroubles Creek primary sewage sludge was fed 20
mL/min butane for a contact. time of 40 uninutes, resulting in a
cumulative butane dose of 800 mL/L. Direct-contact, freeze—thaw
conditioning of primary sewage sludge with butane resulted in a
moderate reduction in specific resistance. 0ther parameters showed
only slight changes. A shift in floc density range was observed; it
was, however, dissimilar to the change in floc density which occurred
upon indirect freezing.
Results of analyses and determinations on samples of primary
sewage sludge conditioned with butane are presented in Table 15.
Particle and Chemical Characteristics - The major effect of
butane conditioning on the particle size distributions of primary
sewage sludge samples was a change in distribution shape. Although,
as can be seen from Table 15, there was little difference in the
total number of particles with mean particle diameter (MPD) less than
250 um, as determined by particle counts, the conditioned sample had
more particles than the unconditioned sample in size ranges with MPD
less than 20 um, and fewer particles in size ranges with larger MPD.
In addition, the conditioned sample had a smaller percentage of
sludge solids retained on a 250-um sieve.
136
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- 'U O UE D 10 CLg,] IZ -¤ O W-I- L/7 ••·· U OQ 1-< O V7 101 U7 Q) 4)( ·)< JJ JJI ^ N 3L) U7 LO O C
3 3 r- ••- •r-
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The quality of the conditioned supernatant sample as evaluated
by particle concentration improved. The distribution of the
conditioned supernatant sample represented fewer particles than that
of the unconditioned supernatant sample in all size ranges, as can be
seen from Figure 18. The number of particles in the size range with
mean particle diameter of 10 um were very close, however, with the
major difference in magnitude noted in size ranges with mean particle
diameter between 15 and 35 um.
The average floc density of primary sewage sludge samples
changed little with butane conditioning, but the distribution of
density was altered. The unconditioned sample had particles ranging
in density from 1.055 to 1.10 g/mL, with most particles forming a
heavy band at 1.045 mg/mL, while particles in the conditioned sample
were concentrated at densities of 1.035 and 1.045 mg/mL. This
narrowing of the range of floc density was in contrast to the
opposite effect resulting from indirect freezing.
Certain changes in particle characteristics, including
deviations from the results of indirect-contact, freeze-thaw
conditioning, can be explained as the influence of rnixing, which
served to mask changes that could be directly attributed to
conditioning.
Dewatering Characteristics - Direct—contact, freeze-thaw
conditioning with butane resulted in a moderate decrease of 22
percent in the specific resistance of primary sewage sludge. Initial
solids content did not increase, as it had for indirectly frozen
138
60000i‘
EJ UNCONDITIONEDQ; O CONDITIONEDE 60000an E3L1J.1L1P-I
E 40000 . SUPERNHTHNTE L!
L1.Ogl 20000 ,„ ¤O 2ZZ3Z 9 Ü __
„10000O•-•x E1 UNCONDITIONED1‘
6000 0 O CONUITIONED(ILul
ß 6000“
3“ 61. 00661; \E 4000 .
2O .2000 “m 2 2E 2 2 _Z 00 10 20 60 40 50 60
MEQN PQRTICLE 0I6METER„ MICRONS
FIGURE 18. PRRTICLE SIZE DISTRIBUTIONS. PRIMHRYSLUDGE CONDITIONED UITH 800 •L1L BUTRNE.
139
sludge. (Initial solids actually showed a slight decrease, but it isprobably that the difference between the conditioned and
unconditioned samples resulted from the difficulty in obtaining a
representative sample.)
The blinding coefficient increased from zero for the
unconditioned sample to a positive value for the conditioned sludge.
However, the blinding coefficient varied from negative to zero to
positive for different samples of unconditioned primary sludge, so
the change may not have been significant.
The effects attributed to mixing and its effects on parameters
of interest were discussed in detail in reporting earlier results of
experiments with waste activated sludge. Like particle changes,
changes in dewatering characteristics caused by conditioning may have
been masked or neutralized by the effects of unixing. while floc
restructuring caused by the freeze-thaw process probably resulted in
reduced specific resistance, the decrease was not accompanied by the
increase in initial dry solids content and strong change in blinding
coefficient that characterized the indirectly frozen sample.
Direct-Contact, Freeze-Thaw Conditioning with Freon 12
A 1-L sample of Stroubles Creek primary sludge was subjected to
1—stage batch conditioning with 250 mL/L Freon. The main effect of
direct-contact freeze-thaw conditioning with Freon 12 on primary
sewage sludge was a large increase in specific resistance, Other
measurable changes in dewatering and particle characteristics were
140
small, with the exception of a large increase in the total number of
particles in the supernatant.
Results of analyses and determinations on samples of primary
sewage sludge conditioned with Freon 12 are presented in Table 16.
Particle and Chemical Characteristics - There was little change
in sludge particle size distributions of primary sewage sludge
samples conditioned with Freon 12, as can be seen from Figure 19. As
can be seen from the data presented in Table 16, the total numbers of
particles with mean particle diameter (MPD) less than 250 um for the
conditioned and unconditioned samples were similar. As for the
butane-conditioned sludge, however, the number of particles in the
Freon-conditioned sample in the size ranges with MPD less than 20 um
was greater than that in the unconditioned sample, and smaller in
size ranges with larger mean particle diameter. As for
butane-conditioned samples of primary sludge, this change probably
resulted from combined effects of freeze-thaw conditioning and
mixing.
0ddly, the supernatant from the conditioned sample had an
excessively large number of particles, about 10 times that of the
unconditioned sample, reflected in all size ranges of the
distribution.
As it had for indirect-contact, freeze-thaw conditioning with
butane, the range of floc densities of sludge conditioned with Freon
12 increased from a single band at 1.03 g/L, to two bands at 1.02 and
1.04 g/mL. This change, similar to that noted for indirect freezing
141
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„ 100009. 0><1*
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“I1.O 0 EQ ZÜÜULu .
‘!Q 3E = “ —-z 00 10 20 30 40 50 60
MEHN PQRTICLE DI8METER„ MICRONS
FIGURE 13. PFIRTICLE SIZE DISTRIBUTIONS. FREON-CONDITIONED PRIMRRY SLUDGE (BFITCH EXPERIMENTS1
143
of primary sludge samples, was the only indication that some
conditioning effect had occurred.
Dewatering Characteristics - There was a threefold increase in
specific resistance with conditioning, from 7100 to 23000 x 1011
m/kg. The general resistance to dewatering, evidenced by the
decrease in both rate and extent of filtration, may have been caused,
in part, by the increased number of small particles in the
supernatant, which is generally recognized as a factor in poor
response to dewateringg. Since mixing was minimal in batch
experiments, it is likely that these small particles were generated
by the freeze-thaw process.
Neither the conditioned nor the unconditioned sample produced a
cake upon vacuum filtration, while centrifuged solids decreased
slightly (less than 10 percent) with Freon addition.
STROUBLES CREEK PRIMARY SEWAGE SLUDGE/WASTE ACTIVATED SLUDGE MIXTURES
Unconditioned samples of a 50/50 mixture of Stroubles Creek
primary sewage sludge and waste activated sludge showed dewatering
characteristics similar to those of primary sludge. Specific
resistance was high, and no cake formed upon vacuum filtration,
Polymer Conditioning
Samples of a 50/50 mixture of Stroubles Creek primary sewage and
waste activated sludges were conditioned with 10, 30, and 50 mg/L
Betz 1160. Polymer conditioning of the sludge mixture resulted both
144
in greatly decreased specific resistance and in cake formation upon
vacuum filtration. The major effect of polymer addition on particle
characteristics was an increase in floc size and a small increase in
floc density.Results of analyses and determinations on mixtures of Stroubles
Creek sludges are presented in Table 17.
Particle and Chemical Characteristics - Polymer conditioning
increased the size of flocs constituting the mixture of Stroubles
Creek primary sewage and waste activated sludges. As can be seen
from Table 17, the total numbers of particles with mean particleC
diameter (MPD) less than 250 pm decreased with increasing polymer
dose, as did the percent of sludge solids passing through a 250-pm
sieve. The distributions for all sludge samples, conditioned and
unconditioned, were similar in shape, with samples conditioned with
increasing polymer doses having fewer particles in each size range.
The same held true in general for the supernatant samples.
Floc density distributions shifted to represent increased
average densities for polymer—conditioned solids. Particles in the
unconditioned sample banded at densities of 1.02 and 1.04 g/mL.
Samples conditioned with 30 and 50 mg/L showed a slight increase in
particle density, with particles banding at 1.03 and 1.05 g/mL. The
particles in the sample conditioned with 50 mg/L concentrated in a
single band at 1.04 g/mL.
Dewatering Characteristics - The specific resistance of mixtures
of Stroubles Creek primary sewage and waste activated sludges was
145
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greatly reduced by polymer addition, and in contrast to the
unconditioned samples, conditioned samples formed a cake upon vacuum
filtration. Centrifuged solids concentrations decreased slightly.
It is interesting to note that while sludge specific resistance
continued to decrease with increasing polymer dose, the corresponding
cake solids concentration decreased slightly. This decrease was
thought to be related to incorporation into the floc structure of
previously free water by the amalgamation of flocs. (This concept
was introduced and discussed in reporting results of experiments with
waste activated sludge.)
The change in the blinding coefficient from positive to
negative, considered in conjunction with the particle size increase,
suggested that small, potentially cake-blinding particles were
coagulated by the polymer into large, more homogenous flocs.
Indirect-Contact, Freeze—Thaw Conditioning
Indirect-contact, freeze—thaw conditioning resulted in major
changes in the dewatering characteristics of a sample of a 50/50
mixture of Stroubles Creek primary sewage and waste activated
sludges. Sludge specific resistance was substantially reduced, and a
cake of moderate solids content formed upon vacuum filtration.
Indirect freezing increased both the characteristic size and density
of sludge particles.A
Results of analyses and determinations on the indirectly frozen
sample of the sludge mixture are presented in Table 18.
147
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Particle Characteristics - Indirect-contact, freeze—thaw
conditioning of a mixture of primary sewage and waste activated
sludges resulted in a shift to larger particle size. As can be seen
from particle totals in Table 18, the number of particles with mean
particle diameter (MPO) less than 250 um decreased, and,
correspondingly, the weight fraction of sludge solids retained on a
250-um sieve increased. The reduction in particle concentration with
conditioning spread across the particle size distribution (Figure
20), with the conditioned sample having fewer particles than the
unconditioned sample in each size range.
The density distribution of sludge mixture flocs changed with
conditioning. Flocs from the unconditioned sample concentrated at
1.04 g/mL, while conditioned flocs were divided into a light band at
1.05 mg/mL and a heavy band at 1.07 g/mL. The increase in average
density and widening of range were also noted for indirectly frozen
samples of primary sludge.
Supernatant TOC increased substantially with conditioning from
31 to 152 mg/L, while pH decreased from 7.6 to 6.7. The changes in
supernatant TOC and sludge pH suggested, as mentioned in reporting
results of experiments with other sludges, that the freeze-thaw
process disrupted existing flocs, resulting in the release of
intrafloc components.
Dewatering Characteristics — Indirect-contact, freeze-thaw
conditioning of the mixture of primary sewage and waste activated
sludges resulted in a nmch improved response to vacuum-filtration.
149
10000 uT} [I1 UNCONOITIONE0
8000 O CONOITIONE0QU')LuÖ 6000 N1: SUPERNFITQNTCZ 0Q¤ 4000Q 0OCI c 0
ä 2000EE ° „ = _
0 '=„10000
O—-•x E1 UNCONDITIONED
nä 8000 CD CONDITIONEDQuJQ[LB 6000 H;,·' 61.0061:O-O
4000QL!
LL uOQ; 2000 ÜLnl 0ß EE = .. = ..Z
0_:::l..22_.__;0
10 20 30 40 60 60MEQN PQRTICLE 0IQMETER• MICRONS
FIGURE 20. PFIRTICLE SIZE DISTRIBUTIONS. INDIRECT-CONTFICT FREEZE-THFIU CONDITIONED PRIMRRY SEVFIGEUFISTE FICTIVRTED SLUOGE MIXTURE.
~ 150
The conditioned sampled dewatered with little resistance toia cake of
moderate solids content. Conditioning reduced specific resistance to
less than 10 percent of its value for the unconditioned sample, from
1500 to 130 x 1011 m/kg. The cake formed upon vacuum filtration was
24 percent solids, significantly higher than that produced with any
polymer dose. (Centrifuged solids concentration, on the other hand,
decreased 41 percent, from 13 percent solids for the unconditioned
sample to 8 percent solids for the conditioned sample.)
These improvements, as well as the reversal of the blinding
coefficient from a positive to a negative value, were attributed to
the changes in floc structure drawn from the particle data. Freezing
produced a denser, larger floc structure. This in turn resulted in a
greater amount of water being outside the floc in the free water
fraction, where it was drained more rapidly via vacuum filtration.
Direct-Contact, Freeze-Thaw Conditioning with Freon 12
Samples drawn from two mixtures of equal volumes of Stroubles
Creek primary sewage and waste activated sludges were direct-contact
freeze-thaw conditioned with Freon 12. The mixtures differed in
solids content because of daily variablity in the primary sewage
sludge. The first sludge mixture ("A"), with an initial dry solids
concentration of about 1 percent, was subjected to 250 mL/L Freon 12
administered in a one-stage batch experiment. The second sludge
mixture ("B"), with an initial dry solids concentration of about 3
percent, was subjected to Freon doses of 250 mL/L and 500 mL/L in
151
one- and two-stage batch experiments, respectively.
The primary effect of Freon conditioning on these sludge
mixtures was an increase in specific resistance. The main change in
particle characteristics was an increased number of small particles
and an increase in the range of floc densities. These changes were
likely caused by a combination of conditioning and mixing effects.
The results of analyses and determinations on 1-liter samples of
these 50/50 mixtures of Stroubles Creek primary and waste activated
sludges are presented in Table 19.
Particle Characteristics - In general, Freon conditioning
increased the concentration of small sludge particles in the primary
sewage/waste activated sludge mixture. As can be seen from Table 19,
the concentration of particles with mean particle diameter (MPD) less
than 250 um increased for each conditioned sample, although this
increase was negligible for sludge mixture A. As a rule, the
conditioned samples had more particles in the size ranges with mean
particle diameter less than 20 pm, and fewer particles in size ranges
with larger mean particle diameter (Figure 21). Otherwise, the
particle size distributions for the conditioned and unconditioned
samples were similar in shape. There was an increase with
conditioning in the weight fraction of sludge solids retained on a
250-um sieve for sludge mixture A, and a decrease for sludge mixture
B.As
reported for other freeze—thaw experiments with primary
sludge and primary/waste activated sludge mixtures, changes in floc
152
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FIGURE 21. PFIRTICLE SIZE DISTRIBUTIONS. FREON-CONDITIONEDPRIMRRY SEHFIGE/URSTE HCTIVFITED SLUOGE MIXTURE(BHTCH EXPERIMENTS1
155
density for sludge mixture A indicated increased heterogeneity in
floc characteristics. while flocs in the unconditioned sample
concentrated at a single density, flocs from the conditioned sample
separated into two distinct bands. The unconditioned sample of
sludge B already showed a range of floc densities, and there was no
observable change with conditioning. The difference in the
characteristic floc density profile for the two mixtures probably
stemmed from the varying ratio of solids contributed by the primary
fraction, with inixture B, having the larger percentage of° primary
solids, showing the greater variation in floc density.
The supernatant from conditioned sludge mixture A had an
excessively high number of particles in each size range (Figure 21),
with almost nine times the total number of particles when compared to
the unconditioned sample. Supernatant TOC also increased. These
results were similar to those reported for Freon-conditioned primary
sludge, and seemed to point to combined effects from inixing and
conditioning. The increase in the number of small particles in
sludge inixture /\ outweighed the potential benefits of' the general
increase in particle size, as evidenced by the increase in the weight
fraction of larger particles for sludge mixture A.
Dewatering Characteristics - Direct-contact, freeze—thaw
conditioning of samples of the mixture of primary sewage and waste
activated sludge with Freon 12 resulted in large increases in
resistance to dewatering. Specific resistance values increased with
conditioning from 1500 to 4000 x 1011 m/kg for the sludge mixture A
156
sample, and from 2900 to 11000 and 15000 x 1011 m/kg for the sludge
mixture B one- and two—stage samples, respectively. Neither the
conditioned nor the unconditioned sample produced a cake upon vacuum
filtration, while centrifuged solids decreased slightly with
conditioning.
As for Freon-conditioned primary sludge, deterioration of
dewatering characteristics could be ascribed to higher particle
concentrations in the supernatant resulting from conditioning.
RAAP ALUM SLUDGE
Unconditioned samples of undiluted RAAP alum sludge dewatered to
high solids concentration upon vacuum filtration and centrifugation,
although they were moderately resistant to filtration. It was
anticipated that polymer addition would improve filtration rate, and
that freeze-thaw conditioning might improve both rate and extent of
dewatering.
Effects of Dilution
Diluting different sludges has been observed to induce varying
effects on dewatering characteristics. Ademiluyi et_al.l2 found that
specific resistance increased or decreased with increasing dilution,
depending upon the sludge type and specific range of solids_
concentration. For example, specific resistance gradually increased
for domestic sewage sludge diluted from 7 percent to 3 percent
157
solids, and then decreased rapidly at higher dilutions. water
treatment plant sludge, in contrast, showed a decrease in specific
resistance ·for dilutions frmn 8 to 3 percent solids, and then an
increase at higher dilutions. It; was speculated that at certain
concentrations, conditions were favorable for release of fine
particles, which then blinded the sludge upon filtration.
In this study, certain samples of RAAP alum sludge was diluted
approximately 3 to 1 with tap water prior to conditioning to reduce
solids concentration to about one percent. Dilution had little
effect on the dewatering characteristics of unconditioned sludge.
Specific resistance remained moderate, and the sludge samples
dewatered to a high dry solids concentration. The sludge showed no
tendency towards cake blinding, either with cn· without dilution.
Particle size distributions varied, but there was no evidence of an
increase in the number of smaller particles with dilution.
Polymer Conditioning
Samples of undiluted RAAP alum sludge were polymer-conditioned
with 50, 75, 100, and 125 mg/L Betz 1160. Polymer addition resulted
in substantial decreases in specific resistance and in slight changes
in dewatered solids concentration. Likewise, increases in the
characteristic size and density of sludge flocs were also observed.
The results of analyses and determinations on
polymer-conditioned samples of undiluted RAAP alum sludge are
158
presented in Table 20.
Particle and Chemical Characteristics - The main effect of
polymer conditioning on particle characteristics <rf undiluted alum
sludge was an increase in particle size. As can be seen from Table
20, the weight fraction of sludge solids retained on a 250-um sieve
increased, and the number of particles with mean particle diameter
(MPD) less than 250 um decreased. This shift towards larger particle
size was also apparent across the size ranges represented by the
particle size distributions depicted in Figure 22. For polymer doses
of 100 mg/L and less, there was a decrease in the number of particles
with MPD less than 20 pm, and an increase in the number of particles
with MPD greater than 20 um.
The 125 mg/L dose seemed to represent a threshold value for
substantive conditioning. The total number of particles per mL with
MPD less than 250 um decreased sharply while the weight fraction of
sludge solids retained on a 250-um sieve increased to 75 percent.
Like particle size, floc density increased substantially with
polymer conditioning. Mass balance calculations indicated that the
increase reflected a 20 percent loss of floc water. Floc structure
observed during floc density analyses also changed. The small,
uniform flocs observed in unconditioned sludge were replaced by
large, bulky aggregates.
The polymer could have caused the apparent release of floc water
by reducing surface charge, thus permitting particles to draw closer
together, and/or by physically trapping particles in a more tightly
159
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10 20 30 40 50 60MEHN PQRTICLE 0lF1METER„ MICRONS
FIGURE 22. PRRTICLE SIZE 0ISTRIBUTIDN.UNDILuTEDPOLYMER-CONDITIONED FILUM SLUDGE.
161
packed structure. water originally measured as integral to the floc
would have been displaced as particles drew, or were drawn, closer
together.
Dewatering Characteristics - Changes in dewatering
characteristics of polymer-conditioned samples of alum sludge were
typical. Large decreases in specific resistance were observed, while
improvements in dewatered cake solids concentration were slight.
Polymer conditioning resulted in only small changes in
vacuum—filtered solids concentration. The unconditioned sample had a
final cake solids concentration of 20 percent; the greatest
improvement, noted for the sample conditioned with 100 mg/L polymer,
was a 15 percent increase to 23 percent solids.
The specific resistance of all polymer-conditioned samples was
reduced by at least 63 percent, to values of 85 x 1011 m/kg or less,
when compared to the unconditioned sludge, which had a specific
resistance of 230 x 1011 m/kg. Reductions in specific resistance did
not vary with polymer dose, nor with the number of particles with MPD
less than 250 um, although there did appear to be a general inverse
relationship between specific resistance and the weight fraction of
sludge solids retained on a 250-pm sieve.
Effects of Dilution - Samples of diluted RAAP alum sludge were
conditioned with 10, 50, and 100 mg/L Betz 1160. Polymer
conditioning resulted in decreased specific resistance at all
doses.Vacuum-filteredcake solids concentration remained stable, except at
the highest polymer dose, where it decreased, while centrifuged
162
solids concentration increased slightly for all polymer doses.
Floc density and particle size increased with increasing polymer
dose. The largest change in particle characteristics was the sharp
decrease in the number of small particles in the supernatant.
Results of analyses and determinations on samples of diluted
alum sludge conditioned with polymer are presented in Table 21.
As can be seen from Figure 23, a major effect of polymer
addition on the particle characteristics of diluted alum sludge was
the decrease in the number of particles with mean particle diameter
(MPU) of 10 pm. Particle size shifted towards more particles in the
25 to 35 pm range for the 10 and 50 mg/L polymer doses. As can be
seen from Table 21, the 100 mg/L dose resulted in a more definite
shift towards larger particles, with the weight fraction of sludge
solids retained on a 250-um sieve increasing from zero for the
unconditioned sample to 50 percent.
The unost striking result of polymer conditioning was in the
reduction of the number of particles in the supernatant.
Concentrations dropped at least two order of magnitude for all
polymer doses, to less than 4 percent of the numbers in the
unconditioned samples.
The 100 mg/L dose produced substantially different results in
other areas as well. whereas TOC had decreased and the floc density
and sludge pH had remained virtually unchanged for lesser doses, the
sample treated with 100 mg/L polymer showed an increase in TOC and
floc density, and a decrease in pH.
l 163
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FIGURE 23. PRRTICLE SIZE DISTRIBUTIONSUILUTEDPOLYMER-CONDITIONED FGLUM SLUDGE.
165
The effects of polymer conditioning on the dewatering
characteristics isf samples of diluted aluni sludge iwere similar to
those observed for undiluted sludge. There was a large decrease in
specific resistance for all polymer-conditioned samples, while
variations in dewatered solids concentrations were small.
Specific resistance decreased to approximately the same level at
each polymer dose, from an unconditioned value of 160 x 1011 m/kg to
13 x 1011 m/kg and less for conditioned samples.
Indirect-Contact, Freeze-Thaw Conditioning
Indirect—contact, freeze-thaw conditioning greatly improved the
dewatering characteristics of undiluted RAAP alum sludge,
outperforming polymer conditioning in all areas. Specific resistance
decreased greatly, while vacuum-filtered and centrifuged solids
concentrations increased 200 and 150 percent, respectively.
Decreased specific resistance was associated with large, concommitant
increases in particle size and floc density.
The results of analyses and determinations for an indirectly
frozen sample of undiluted RAAP alum sludge are presented in Table
22.Experimental Observations - Thawed alum sludge solids had the
granular, gritty appearance typical of freeze-thaw conditioned
sludge. A large amount of supernatant was decanted from the product
sludge, resulting in a fivefold increase in initial dry solids
content.6
166
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Particle and Chemical Characteristics - The large increase in
particle size resulting from indirect—contact, freeze-thaw
conditioning of undiluted alum sludge was apparent from the large
amount of sludge solids retained on a 250-um sieve for the
conditioned sludge. No measurable fraction was retained upon sieving
the unconditioned sample, while 76 percent of the conditioned sludge
solids fell in this size range.
The similarities in distributions of particles with mean
particle diameter (MPO) less than 250 pm (Figure 24), as well as the
total number of particles represented by these distributions, for
conditioned and unconditioned samples were belied by comparison of
the weight fractions of total sludge solids that the distributions
represented. The particle distribution depicted for the
unconditioned sample represented approximately 100 percent of sludge
solids, while the distribution depicted for the conditioned sample
represented a much smaller fraction of solids--—approximately 24
percent-—-from a more concentrated sludge. The number of particles
in these size ranges would have decreased with conditioning, had
supernatant not been removed from the sample, thereby increasing
initial solids content.
Floc density increased greatly with conditioning, from 1.17 g/mL
to more than 1.3 g/mL, representing the release of up to 46 percent
of floc water.
Dewatering Characteristics - Indirect-contact, freeze-thaw
conditioning of undiluted alum sludge resulted in large increases in
168
15000 ·11 Q] Ü UNCÜNÜITIONEÜQ 12000 1 O CÜNDITIONEÜE \U') ••u..I.1U 9000
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Em 3000 'ZE c
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00.
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, Z :D 2 X: ·~Z 0 gä"-20 10 20 90 40 S0 60
MEHN PQRTICLE DI9METER„ MICRONS
FIGURE 2%. PHRTICLE SIZE DISTRIBUTIONS. UNDILUTED INDIRECT-· CONTFICT FREEZE-THHH CDNDITIONED FILUM SLUDGE.
169
initial and dewatered solids concentrations and a large decrease in
specific resistance. Initial solids content increased 450 percent,
from 3.2 to 14.7 percent solids. Conditioned vacuum-filtered cake
solids concentration nearly doubled, from 21 percent solids for the
unconditioned sludge to 40 percent solids. Centrifuged solids almost
tripled, from 10 to 26 percent. The change in specific resistance
was correspondingly large, with a decrease from 190 x 1011 m/kg for
the unconditioned sample, to less than 1 x 1011 m/kg for the
conditioned sample.
These results were the classic response to indirect-contact,
freeze-thaw conditioning: a dramatic increase in particle size and
density, accompanied by large improvements in specific resistance and
in initial and dewatered solids concentration. All evidence
indicated that a large amount of water previously unavailable for
removal was released by the freeze-thaw process, and that the removal
of this water, reduction of surface charge, compression or rupture of
particles, and/or other changes resulting from the freeze-thaw
process, enhanced the formation of large, dense flocs with remarkable
settling and dewatering properties.
Effects of Dilution - The dewatering characteristics of diluted
RAAP alum sludge were greatly improved by indirect-contact,
freeze-thaw conditioning. Specific resistance was reduced to less
than one percent of its initial value, and there were large increases
in initial and dewatered solids concentrations. Floc density and
particle size increased, and there was a large reduction in the
170
number of particles in the supernatant.T
The results of analyses and determinations for an indirectly
frozen sample of RAAP alum sludge diluted to one percent are given in
Table 23.
The main change in particle characteristics, as can be seen from
Table 23, was an increase in the percent of sludge solids larger than
250 um. Approximately 78 percent of the conditioned sludge solids
were retained on a 250-um sieve, as compared to none for the
unconditioned sample. Particle size distributions, while apparently
similar, as can be seen from Figure 25, were fundamentally different,
in that the initial solids concentration of the conditioned sludge
was 15 times that of the unconditioned sludge. These results were
similar to those observed for undiluted sludge. Initial solids for
conditioned samples of diluted and undiluted sludges were practically
identical, as were weight fractions of solids retained on a 250-um
sieve.
Supernatant distributions for the two samples were also quite
different. There were very few particles in the indirectly frozen
supernatant sample, less than five percent of the total number of
particles counted for the unconditioned sample. In contrast, the
undiluted sludge had shown no such improvement. Also, conditioning
of diluted sludge resulted in a moderate decrease in supernatant TOC,
from 2O to 8 mg/L, while there had been no improvement for undiluted
sludge.
The changes in dewatering characteristics of diluted alum sludge
I7I
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FIGURE 25. PRRTICLE SIZE DISTRIBUTIONSDILUTED INDIRECT-CONTFICT FREEZE-THRU CONDITIONED RLUM SLUDGE.
173
with indirect-contact freeze-thaw conditioning were striking, as they
had been for the undiluted sludge. The increases in solids
concentration, both initial and dewatered, for the indirectly frozen
sample of diluted alum sludge were very large. Initial dry solids
concentration increased from 1 to 15 percent. Vacuum-filtered cake
solids concentration‘ nearly doubled with conditioning, from 22
percent dry solids for the unconditioned sample to 41 percent dry
solids for the indirectly frozen sample. Centrifuged dry solids
concentration nearly tripled, from 10 to 28 percent dry solids. The
specific resistance of the sludge decreased sharply following
freeze-thaw conditioning.
Direct-Contact, Freeze-Thaw Conditioning with Butane
One-L samples of undiluted RAAP alum sludge were conditioned
with 20 mL/min butane for contact times of 20, 30, and 40 minutes,
resulting in butane doses of 400, 600, and 800 mL/L, respectively.
The only improvement noted in dewatering characteristics was a slight
increase in vacuum-filtered solids concentrations at the highest
butane dose. Specific resistance increased to similar values for all
conditioned samples. The only consistent change in other parameters,
including particle characteristics, was a moderate decrease in pH.
Results of analyses and determinations on samples of
butane-conditioned, undiluted alum sludge are presented in Table 24.
Experimental Observations - The butane conditioning process
generated large amounts of foam in alum sludge samples. In general,
y 174
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the foam had a higher initial solids content (about 4 percent) and
dewatered to a lower vacuum-filtered solids concentration (about 20
percent) than either the unconditioned or conditioned sludge.
Particle Characteristics - Changes in particle characteristics
varied considerably and inconsistently; there were no general trends
observed which could be related to increasing butane dose. The cause
of certain changes were suggested by the results of previous
experiments with other types of sludge.
There was little change in the distribution of particles with
mean particle diameter (MPD) less than 50 um for the sample
conditioned with 400 mL/L butane (Figure 26), and the total number of
particles per mL with MPD less than 250 pm also remained about the
same. However, the weight fraction of sludge solids retained on a
250-pm sieve increased slightly and the floc density distribution
narrowed, shifting towards a typically more dense particle. The
changes in floc density and weight fraction reflected an increase in
the percentage of larger, more dense particles, suggesting that some
freeze-thaw conditioning might have occurred.
The changes in the particle characteristics of the undiluted
alum sludge sample conditioned with 600 mL/L (Figure 27), while
different from those resulting from the 400 mL/L dose, also indicated
that certain freeze—thaw effects might have occurred. Initial solids
content more than doubled, accounting for a certain part of the~
increase in the total number of particles per mL with MPD less than
250 pm. Although most of the increase was in the size ranges of MPD
( 177
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[E1 UNCONDITIONEDC) CONDITIONED
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FIGURE 26. PRRTICLE SIZE DISTRIBUTIONS. UNDILUTED RLUMSLUDGE CDNUITIONED WITH *00 ••L/L BUTHNE.
178
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FIGURE 27. PRRTICLE SIZE DISTRIBUTIONS. UNDILUTED m.uMSLUDGE CONDITIONED WITH 600 •L/L BUTGNE. .
179
of 10 um or less, suggesting mixing-related changes, particle
compression may have been responsible for a fraction of these smaller
particles. The supernatant also contained a large number of small
particles, most with MPD less than 10 pm.
The only noticeable change in particle characteristics for the
sample conditioned with 800 mL/L butane was a decrease in the amount
of solids retained on a 250-um sieve, which may have resulted from
the production of fines through freezing.
Dewatering Characteristics - The effects of butane conditioning
on the dewatering characteristics of alum sludge were variable, with
certain changes in dry solids concentration obtained upon vacuum
filtration and centrifugation and increases in specific resistance.
For butane doses of 400 and 600 mL/L, there was a small increase and
decrease, respectively, in vacuum-filtered cake solids concentration,
while cake solids concentration increased 13 percent for the 800 mL/L
dose. Centrifuged dry solids concentration of the sample conditioned
with 400 mL/L butane showed a large (perhaps anamolous) increase, but
did not change for the sample conditioned with 600 mL/L butane, and
decreased for the 800 mL/L dose.
Changes in specific resistance with butane conditioning were
more consistent, as shown in Figure V28. Specific resistance
increased for all butane-conditioned samples, from 160 to 170 x 1011
m/kg for the unconditioned samples, to more than double that value.
Conditioning had no effect on the sign of the blinding coefficient,
which was negative for all samples.
180
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0 0 200 400 800 800 1 000BUTHNE 00SE. LLL/L
FIGURE 28. SPECIFIC RESISTRNCE V5 BUTRNE 00SE.UNDILUTED BUTRNE-CONOITIONE0 RLUM SLUDGE.
181
Contact times for these experiments were relatively short and
the degree of freezing taking place indeterminate. This may explain
the absence of any clear trends. The large increase in floc density,
in the number of particles with MPD greater than 250 pm, and in
centrifuged solids concentration for the sample treated with 400 mL/L
butane, and the increase in initial solids concentration for the
sample treated with 600 mL/L may have been indications of the
conditioning effect of the freeze-thaw process. As suggested in
reporting results of earlier experiments, the vacuum filtration
process might have been more sensitive to interference from the foam
generated during application of the butane, thus explaining the
limited response in vacuum filtered solids and the increase in
specific resistance. Improvement may also have been obscured by the
detrimental effects of mixing.
The only trend consistent with the results of indirect freezing
was a decrease in sludge pH for all conditioned samples.
Effects of Dilution - A one—liter sample of diluted RAAP alum
sludge was conditioned with 20 mL/min butane for a contact time of 75
min, resulting in a butane dose of 1500 mL/L. This experiment
represented an attempt to determine the effects of larger butane
doses. The results were very similar to those obtained for smaller
doses applied to samples of undiluted sludge. There were slight
increases in vacuum-filtered and centrifuged solids concentrations,Q
while the specific resistance of the sludge doubled. The range of i
floc density increased, while other particle characteristics remained
182
unchanged.
Results of analyses and determinations on samples of
butane-conditioned, diluted alum sludge are presented in Table 25.
Direct-Contact Freeze-Thaw Conditioning with Freon 12
One-L samples of undiluted RAAP alum sludge luere conditioned
with Freon 12 in batch and continuous experiments. In the batch
experiments, samples were treated in one and two stages, with 250 mL
Freon applied at each stage. In the continuous experiment, the
sample was treated with 10 mL/min Freon for a contact time of 50 min.
Thus, the sample treated in the one-stage batch experiment was
exposed to 250 mL/L Freon; and the samples treated in the two-stage
batch experiment and in the continuous experiment were exposed to 500
mL/L Freon.
In general, the application of Freon 12 to undiluted alum sludge
samples had little effect on particle or dewatering characteristics.
Specific resistance increased, whether the Freon was applied
continuously or as a slug dose. The increase in specific resistance
was smaller for batch experiments than for the continuous experiment,
suggesting mixing effects. Vacuum-filtered solids concentration
decreased for all conditioned samples. Centrifuged solids
concentration increased slightly for samples batch-conditioned with
Freon, but decreased for the continuously conditioned sample.
Results of analyses and determinations on samples of undiluted
alum sludge conditioned with Freon are presented in Tables 26 and 27
183
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for batch and semicontinuous experiments, respectively.
Particle Characteristics - Effects of Freon conditioning on the
particle characteristics of samples of undiluted alum sludge were
small. Average floc density increased slightly with Freon addition
in both batch and continuous experiments, while there were no notable
changes in other particle characteristics. Supernatant quality
deteriorated considerably, with an order—of—magnitude increase in the
number of particles with mean particle diameter (MPD) less than
250 um in the supernatant from the sample conditioned in two stages
with 500 mL/L total Freon, and the absence of any removable
supernatant at all from the sample conditioned with 500 mL/L in the
continuous experiment.
Dewatering Characteristics - Freon conditioning of undiluted
alum sludge resulted in slight increases in centrifuged solids for
batch experiments. The response to vacuum filtration, however, was
uniformly poor. Specific resistance increased for all doses and
conditioning regimes, and vacuum-filtered solids decreased. The
continuously conditioned sample failed to form a cake upon
filtration,
A few tenuous relationships can be drawn from the experimental
data. For batch experiments, increased centrifuged solids
T concentrations were accompanied by increases in floc density. This
relationship suggested that the addition of Freon to the sludge had
some conditioning effect. This relationship was not observed for the
semicontinuously conditioned sample, which had an increase in floc
187
density but no change in centrifuged dry solids concentration. Since
this sample was mixed for a much longer time than the
batch—conditioned samples, this results might have been caused by the
detrimenal effects of mixing. It is interesting to note that this
sample was also the only one not to form a cake upon vacuum
filtration, and had the highest specific resistance.
Effects of Dilution ·- 0ne-liter samples of RAAP alum sludge
previously diluted to a 1 percent dry solids concentration were
conditioned with Freon, in batch and continuous experiments. In the
batch experiments, samples were treated with 1-, 2-, and 3-stage
conditioning, with 250 mL Freon applied at each stage. In the
continuous experiments, samples were fed 10 mL/min Freon for contact
times of 25, 50, and 75 rninutes. The samples treated in 1—stage
batch and 25-min continuous experiments were fed 250 mL/L Freon; the
2—stage batch- and 50-min continuously conditioned samples, 500 mL/L;
and the 3-stage batch- and 75-min continuously conditioned samples,
750 mL/L. Results of analyses are presented in Tables 28 and 29 for
batch and continuous experiments, respectively.
Particle size distributions for conditioned and unconditioned
samples of diluted alum sludge were similar in shape and magnitude,
with the exception of the samples batch-conditioned with 500 mL/L
Freon (Figure 29) and continuously with 250 mL/L (Figure 30). These
samples had greater numbers of particles in the size ranges with mean
particle diameter less than 40 um. The total number of particles per
mL represented by the distribution of the batch—conditioned sludge
188
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191
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FIGURE 30. PRRTICLE SIZE UISTRIBUTIUNS. UILUTEO. FREUN-CONDITIUNEU RLUM SLUUGE LCUNTINUOUS EXPERIMENTS1
192
was double that of any other sample.
Floc density increased slightly for batch conditioned samples.
Supernatant TOC increased with conditioning from 10 mg/L for the
unconditioned sample up to 38 mg/L for conditioned samples, with no
trend. The pH of batch-conditioned samples decreased with Freon
dose, from 8.4 for the unconditioned sample to 7.4 for the sample
from the 3-stage experiment, while there were only slight variations
in pH for continuously conditioned samples.
The major effect of Freon conditioning on the dewatering
characteristics of diluted alum sludge was a substantial increase in
vacuum-filtered solids concentration for batch experiments, a change
that was not noted for continuously conditioned samples.
Vacuum-filtered dry solids concentration increased for all
batch-conditioned samples, from 23 percent solids for the
unconditioned sample to 27 to 28 percent solids for conditioned
samples. This change represented 17 to 22 percent increases in
solids concentration. There were only slight variations in final cake
solids concentration for continuously conditioned samples, which
ranged from 23 to 24 percent, as did the final cake solids
concentration for unconditioned samples.
whereas there were only slight variations in specific resistance
values of batch-conditioned samples, there was a clear upward trend
in specific resistance values with increasing contact time for
continuously conditioned samples, as shown in Figure 31. Specific
resistance values increased from 100 to 140 x 1011 m/kg for
193
400
E1 BQTCHC) CONTINUOUS
90°”° 300X
.2*g 1uiUZCEI-LD 200 9I-1U)W asIILJ•-• •:
G I;I.1..I 100 ¤= “ ¤O.U')
ss
0 0 1 00 200 300 400 500 600 700 600FREON DOSE. nL/L
FIGURE 31. SPECIFIC RESISTHNCE V5 FREON DOSE.DILUTED FREON-CONDITIONED FILUM SLUDGE.
194
unconditioned samples, to 270 x 1011 m/kg for the sample
semicontinuously conditioned with 750 mL Freon. This sample had very
poor supernatant quality.O
Dewatering characteristics of undiluted sludge had generally
deteriorated for samples freeze-thaw conditioned with Freon. More
promising results were obtained for diluted sludge, particularly for
those conditioned in batch operation.
195
V. DISCUSSION
The purpose of this study was to develop and evaluate
direct-contact, freeze-thaw processes for conditioning wastewater
and water treatment sludges in the context of conventional
conditioning methods and to develop a theoretical model for the
freeze-thaw process. This chapter presents the following:
- a proposed mechanism for conditioning effects achieved
during freeze-thaw processes, based upon the results of
indirect-contact, freeze-thaw experiments;
- a comparative evaluation of direct-contact, freeze-thaw
conditioning; indirect-contact, freeze-thaw conditioning;
and polymer conditioning; and
- a comparison of the results of the current investigation
with other studies and a discussion of process viability.
PROPOSED MECHANISM FOR FREEZE-THAw CONOITIONING
In reviewing the particle and floc characteristics of sludgesl
treated with direct-contact, freeze-thaw processes, no clear trends
were discovered which could be used independently to formulate a
196
mechanistic explanation of freeze-thaw conditioning. Results
obtained with indirect-contact, freeze-thaw conditioning of the
various sludges used in this study suggested a two-stage mechanism
for conditioning: the disruption of both the sludge floc and
particle structural components, and the formation of a rmw sludge
floc arrangement. The effects of the freeze-thaw process
ondewateringcharacteristics were dependent upon these sludge—specific
changes in particle and floc characteristics.
Disruption of Sludge Structure
The first hypothetical stage in the freeze-thaw process, the
disruption of existing flocs and particles, was evidenced in these
experiments by changes in floc density ranges, in sludge pH, and in
supernatant TOC concentration. The basic conditioning effect of this
stage was the release of water previously incorporated in the
original floc structure.
Changes in floc density indicated that the freeze-thaw process,
at a minimum, altered sludge structure at the floc level. As can be
seen from Table 30, freeze-thaw conditioning resulted in wider
density ranges for certain sludges and in increased average density
for each type of sludge.
The increase in floc density range observed for conditioned
samples containing primary sludge included flocs of lesser and
greater density than the original range. The appearance of less
dense flocs in these samples suggested that the particles
197
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constituting flocs were forced apart from one another during the
freeze-thaw process. The observation of this phenomenon only in
samples containing primary sludge suggested that primary sludge
flocs, characteristically more heterogeneous than either waste
activated or alum sludge, were more susceptible to disruption during
freezing than the other sludges.
Alternatively, changes in floc density range may actually have
occurred in other sludges, but may have been obscured by the
limitations of particle analytical methods, i.e.:
1. The amount of water which must be lost or gained to affect
a measurable change in floc density depends upon the dry
density of the sludge solids. For example, a much larger
amount of water loss is required to increase the floc
density from 1.02 to 1.03 g/mL for a sludge with a dry
density of 1.10 g/mL than for a sludge with a dry density
of 2.0 g/mL. Since waste activated sludge dry solids have
a low characteristic density, a relatively large change in
the amount of water associated with the floc would be
necessary to be reflected by changes in measured floc
density.
2. The density of indirect—contact, freeze-thaw-conditioned
alum sludge flocs was greater than the maximum density that
could be achieved via concentration of the Percol media
199
(maximum density = 1.30 g/mL).
It is also possible that amalgamation of particles in waste activated
and alum sludge samples upon thawing may have obscured fundamental
changes in particle characteristics induced by freezing.
As shown in Table 30, average floc density increased for all
sludges. (Average floc density for each sludge was taken as that
density gradient at which the greatest amount of sludge was
deposited. If sludge was concentrated more or less equally at more
than one gradient, the corresponding densities were averaged to
obtain the mean value.) This densification can be attributed to the
loss of floc water during the freeze-thaw process. To determine the
percentage of floc water hypothetically released, a general mass
balance was written around the floc as:
pf = <¤d„},(pd„y) + <¤w<¤w) [231
where
odry = fraction of floc volume occupied by dry
solids (dimensionless) 2
owet = fraction of floc volume occupied by water(dimensionless)
pdry = dry solids density (g/mL)
pwet = density of water (1.0 g/mL)
Based upon observed changes in floc density conditions, the
200
percentage of floc water released was calculated as:
% released = [Qwu ”©wc(¢dryu/¢dryc)](l00) [24]
Qwu
where the notations "u" and "c" denote unconditioned (control) and
conditioned volume fractions, respectively.
As can be seen from the data presented in Table 30, the
percentage of floc water released by the indirect-contact,
freeze-thaw process varied from 28 to over 50 percent.
Changes in the fundamental chemical characteristics of
conditioned sludges suggested that particles as well as flocs may
have been disrupted by the freezing process. As can be seen from the
data presented in Table 31, changes in sludge pH and supernatant TOC
concentrations were significant. The pH of primary sludge, primary
sludge/waste activated sludge mixtures, and alum sludge decreased,
while the pH of waste activated sludge increased. Changes in
supernatant TOC concentration for primary sludge and for primary
sludge/waste activated sludge mixtures were large, with increases of
over 100 percent.
Due to the described limitations in particle analyses, the
extent and nature of particle disruption is not evident from these
observations. There are at least three mechanisms which may singly
or together be used to explain the data: .
1. Dehydration and Rupture - Mechanical stresses and/or
201
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physical/chemical imbalances produced during freezing could
result in dehydration and rupture of cells and particles.
Discussing the results of his study of butane conditioning
of waste activated sludges, Khan3O hypothesized that large
mechanical stresses placed on the cell during freezing
caused the release of internal water, which subsequently
froze outside the cell. Irreversible changes resulted from
contact of cellular protein formerly isolated by internal
water. Mechanical stress could similarly disrupt
non-biological particles.
Silvares71 found that cells in a slowly freezing
solution are immersed in an increasingly saline
environment. The resulting concentration gradient across
cell boundaries elicits water from the cells, resulting in
cellular dehydration. Ice unay also forna with the cell,
which could ultimately lead to the rupture of cells into
smaller particles30’34.
The occurrence of particle/cell dehydration and
rupture in the current investigation is supported by the
data which indicated increases in floc density range and
average floc density and changes in supernatant TOC
concentration and sludge pH.
2. Particle Compression - The intense pressures generated
during freezing may deform particles without significant
203
loss of water or destruction of cell boundaries. —In
freeze-thaw experiments with water treatment sludges,
Flint78 used X—ray diffraction techniques to determine that
the size of aluminum hydroxide "crystallites" was actually
halved by the process. Flint suggested that the particles
were compressed by the expansion of external freezing
water. In the current study, compression may have enhanced
for the densification of floc observed for all sludges.
3. Change in Particle Surface Charge - Changes in particle
surface charge may also occur upon freezing. Flint78T hypothesized that the readiness with which the aluminum
hydroxide "crystallites" produced by freeze-thaw
conditioning precipitated was due to reduction of surface
charge. The large electric potential which may develop
across the ice-water interface may impart a negative charge
to the liquid surrounding the particles, thereby
neutralizing them. Such changes could also explain in part
the increases in average floc density observed for all
sludges.
Formation of New Floc Structure
Many of the particle and dewatering data collected in this study
support the hypothesis that the second stage in the freeze-thaw
process is the formation of new flocs. whether flocs and particles
204
experienced dehydration and rupture, compression, and/or a change in
surface charge, the basic effects of the freeze—thaw process on the
sludges in this study were large increases in floc density and
particle size. The flocs comprising the conditioned sludge were thus
fundamentally different from those originally constituting the
unconditioned sludge.
The changes in floc density were previously discussed in the
context of floc disruption. Conditioned flocs were, on the average,
considerably denser than unconditioned flocs, as can be seen from
data in Table 30. Large changes also occurred in particle size
distributions for each sludge. Data in Table 32 document the
reductions in the number of particles with mean particle diameter
less than 250 pm per mg of sludge solids for each sludge.
Concentrations of particles (number/mL) were normalized by dividing
by initial solids concentration to account for differences in solids
content among sludges and between conditioned and unconditioned
samples. As can be seen from the data in Table 32, reductions in the
number of small particles per unit weight of sludge solids were
substantial, ranging from 80 to 96 percent.
Increases in the weight percent of particles greater than 250 um
in size were correspondingly large. For unconditioned samples of
waste activated and alum sludges, there was no fraction of particles
retained on a 250-pm screen. with conditioning, the weight percent
retained on a 250-pm screen increased to 73 percent or greater for
each sludge.L
205
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The increases in floc density and particle size suggest that
particles were simply forced together by intense pressure during
freezing ‘u> fomn larger ones, squeezing out excess water. Other
results suggest a inore complex process combining cell disruption,
particle compression, and surface charge reduction, as discussed in
the previous section.
The general effects of the conditioning-induced changes in
particle and floc characteristics were increases in initial and
vacuum-filtered solids concentrations, and variable, sludge—specific
changes in centrifuged solids and specific resistance. Data
included in Table 33 show that the change in initial,
gravity-thickened solids concentration with conditioning was
substantial, with increases ranging from 62 to 1600 percent. This
increase corresponds well with the calculated values for floc water
content lost due to conditioning (Table 30). Much of the floc water
released by the freeze-thaw process completely dissociated from the
floc and was easily drained off as supernatant.
The improvements in dewatered solids concentrations for certain
sludges can also be related to the release of previously bound floc
water. As can be seen from data in Table 33, the solids obtained
following vacuum filtration showed increases of 51 to 90 percent,
where measurable. (Primary sludge and primary sludge/waste activated
sludge mixtures did not produce cakes before conditioning; thus
extent of improvement could not be determined). Indirect freezing
showed increases of 15 to 190 percent in the solids concentration
207
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obtained following centrifugation, except for samples containing
primary sewage sludge. Conditioned samples comprised by or
containing primary sewage showed a decrease in centrifuged solids
concentration. This decrease was assumed to result from the change
in floc density range, with less dense particles remaining suspended
after centrifugation,
Arundel77 investigated the dewatering behavior of sludges
exposed to long—term applications of high pressure. She
characterized both the floc density and the dewatered solids
concentration obtained following high pressure application. The
observed increase in floc density was concluded to be related to floc
deformation and the release of internal floc water. This likewise
correlated to the generation of significantly greater cake solids
concentrations. Likewise, the intense pressures developed during
freezing have been suggested as producing similar water release
during sludge conditioning63’78.
Indirect freezing produced a marked improvementa in sludge
dewatering rate as evidenced by a significant decrease in sludge
specific resistance (data in Table 33). This result was predictable
based upon the increase in the characteristic particle size
distribution observed following conditioning. The only anomaly was
with respect to the conditioning of the waste activated sludge
sample; in this instance, an increase in specific resistance was
observed. The reason for this response was not immediately evident
upon analysis of the sludge characterization data collected.
209
EVALUATION 0F DIRECT-CONTACT, FREEZE-THAW CONDITIONING(
There are three main advantages of direct-contact, freeze-thaw
conditioning processes when compared to indirect-contact processes:
(1) reduced energy requirements, (2) flexibility in reactor
configuration, and (3) maintenance of a pumpable slurry, thus
permitting continuous operation. These advantages must be weighed
against the main disadvantage of direct-contact processes, that is,
the reduced potential for improvement in dewatering characteristics.
The following sections discuss the observed effects of direct-contact
freeze-thaw conditioning on particle, chemical, and dewatering
characteristics and compare them to the results of the
indirect-contact process.
Particle and Chemical Characteristics
The decrease in the number of particles with mean particle
diameter (MPO) less than 250 pm per mg of sludge solids, observed for
all sludges conditioned with the indirect-contact process, provided
evidence of the general increase in particle size and change in floc
structure resulting from this freeze-thaw process. In contrast,
normalized concentrations of particles present in each sludge sample
conditioned with a direct-contact process increased significantly in
comparison to the control sample. (Selected data are presented in
Table 34.) These values reflected an increase in the number of
particles; in fact, most of this increase was due to the production
of very fine ((20 pm) size particles.
210
TABLE 34
EFFECT OF DIRECT-CONTACT, FREEZE-THAW CONDITIONINGON PARTICLE CHARACTERISTICS
No. of Particles With MPD(250 um per mg6of Sludge Solids
Sludge Conditioning Method (x 10 ) Range
Waste Activated (WA) None (Control) 10.4Direct Freeze (Butane) 14.5
None (Control) 18.6Direct Freeze (Freon) 24.3
Primary Sewage (PS) None (Control) 10.6Direct Freeze (Butane) 15.4
None (Control) 17.8Direct Freeze (Freon) 25.7
Alum, Undiluted None (Control) 17.9Direct Freeze (Butane) 28.2
None (Control) 7.4Direct Freeze (Freon) 9.0
Alum, Diluted None (Control) 17.0Direct Freeze (Butane) 18.2
None (Control) 20.9Direct Freeze (Freon) 38.7
211
The general effect of indirect—contact, freeze-thaw conditioning
on measured sludge floc characteristics was an increase in the
average sludge floc density. For certain sludges (alum sludge, in
particular), this increase was large. In contrast, minimal changes
in floc density ranges and averages for both butane- and
Freon-conditioned sludges were observed. The direction of change
varied, as can be seen from the selected floc density data presented
in Table 35. Two trends were noted:
1. Average floc density increased for alum sludge conditioned
with Freon, as it had for sludges conditioned with the
indirect-contact process.
2. Floc density range increased for all sludges
batch-conditioned with Freon, as it had for
indirect-contact conditioned samples consisting totally or
partially of primary sludge. The latter was interpreted as
a sludge-specific phenomenon, as the increase was not
observed for other sludges. In this case, the result
appeared to be refrigerant-specific.
Changes in sludge pH were observed in sludges conditioned with
the indirect-contact process. These changes were interpreted to
signal disruption of the sludge at the primary particle level.
Similar changes were noted in butane- and Freon—conditioned samples
212
TABLE 35
EFFECT DF FREON CONDITIONINC ON FLOC CHARACTERISTICS
~Floc Density g/mL
Sludge Conditioning Method Average Range
Waste Activated (WA) None (Control) 1.035 1.03 — 1.04Direct Contact (Freon) 1.02 1.01 - 1.05
Primary Sewage (P5) None (Control) 1.03 ·Direct Contact (Freon) 1.03 1.02 - 1.04
WA/PS Mixture None (Control) 1.04 -Direct Contact (Freon) 1.04 1.03 - 1.05
Alum, Undiluted None (Control) 1.17 1.16 - 1.18Direct Contact (Freon) 1.18 1.16 - 1.18
Alum, Diluted None (Control) 1.17 1.16 - 1.18Direct Contact (Freon) 1.18 -
213
of alum sludge. Minimal change in pH was noted for other sludges.
Moderate changes in supernatant TOC were also observed in
sludges conditioned with the indirect-contact process. In general,
increases of similar magnitude to these changes occurred for sludges
conditioned with the direct-contact process. Two deviations were
noted. First, the supernatant TOC concentration of the waste
activated sludge conditioned with 400 mL/L butane was several times
greater than the supernatant TOC concentration for any other
conditioned or unconditioned waste activated sludge sample. Also,
the supernatant TOC concentration of certain butane- and
Freon—conditioned alum sludge samples increased, whereas there had
been no such increase for the samples conditioned with the
indirect-contact process.
As suggested in the presentation of results, these increases may
have been caused by the suspension of fines in the supernatant as a
result of mixing. Butane-conditioned supernatant samples might also
have contained significant concentration of dissolved or emulsified
butane. For example, based upon butane solubility at experimental
temperatures, up to 50 percent of the total increase in TOC
concentration noted for the waste activated sludge sample treated
with 400 mL/L butane could be attributed to solubilized butane. All
or part of the remaining increase could be accounted for by the
presence of emulsified butane in the supernatant, which has been
reported in amounts up to ten times that of dissolved butane in
freeze—thaw process products26.
214
DewateringCharacteristicsThe
indirect-contact, freeze-thaw process generally resulted in
higher cake solids concentrations and 'lower specific resistance
values for the sludges studied. As for changes in particle
characteristics, the direct-contact processes resulted in variable
changes in dewatering characteristics, usually of lesser magnitude.
Initial and vacuum-filtered solids concentrations obtained upon
indirect-contact, freeze-thaw conditioning were typically higher than
those noted for unconditioned samples. Similar results were noted in
solids concentrations of certain sludges conditioned with
direct-contact processes. Selected results are presented in Table
36.
Certain samples of butane- and Freon-conditioned alum sludge and
butane-conditioned waste activated sludge showed slight increases in
initial solids concentration. The dewatered solids concentrations of
certain samples of waste activated and diluted alum sludges
conditioned with direct-contact processes improved,
Changes in specific resistance with indirect-contact,
freeze-thaw conditioning were sludge specific. The specific
resistance of alum and primary sewage sludges and of primary
sewage/waste activated sludge mixtures greatly improved, while
increasing with indirect-contact conditioning for waste activated
sludge. In contrast, specific resistance deteriorated for almost
every sludge sample conditioned with a direct-contact process.
(Selected data are presented in Table 36.) The exceptions were
215
TABLE 36
EFFECT OF DIRECT-CONTACT, FREEZE—THAW CONDITIONINGON DEWATERING CHARACTERISTICS
Solids SpecificConcentration, % Resistance,
Sludge Conditioning Method Initial Vacuum·Filtered m/kg x 10
Waste Activated (WA) None (Control) 1.0 12.9 36Direct Contact (Butane) 1.2 13.3 290
None (Control) 0.8 8.3 210Direct Contact (Freon) 0.6 13.5 360
Primary Sludge (PS) None (Control) 2.1 · 4,100Direct Contact (Butane) 1.4 - 3,200
None (Control) 1.5 - 7,100Direct Contact (Freon) 1.1 - 23,200
Alum, Undiluted None (Control) 1.3 24.0 160Direct Contact (Butane) 2.8 23.7 290
None (Control) 3.3 16.1 150Direct Contact (Freon) 3.6 13.1 260
Alum, Diluted None (Control) 1.1 21.3 125Direct Contact (Butane) 1.2 23.1 205
None (Control) 0.8 23.4 110Direct Contact (Freon) 0.8 28.0 120
216
butane—conditioned primary sludge, for which there was an
improvement, and Freon-batch—conditioned alum sludge, for which there
was virtually no change in specific resistance with conditioning.
The increases in specific resistance, which were very
significant in certain instances (for example, the Freon-conditioned
primary sludge), were probably due to the production of large numbers
of very fine particles during conditioning and to the foam and scum
layers typically generated during the direct-contact process.
In summary, the benefits observed from indirect-contact
conditioning, such as particle compression, increased floc density,
higher cake solids concentrations, and lower specific resistance
values, were not generated by the direct-contact processes. A
combination of causes is likely responsible for these results,
including the rate and extent of freezing and process-specific
factors, such as mixing and foaming.
The rate of freezing was relatively rapid in the direct-contact
experiments. The detention time for freezing was typically less than
45 minutes, with virtually instantaneous freezing occurring in
certain instances (i.e., batch conditioning with Freon). In
comparison, in the indirect-contact process, solid freezing occurred
over two to four hours.
Other researchers have noted that the rate of freezing affects
sludge characteristics. Logsdon and Edgerly63 found that slow
freezing permitted development of elongated, crystalline solids,
which drained well upon thawing. Rapid freezing resulted in small
217
ice crystals enveloped by a matrix of dissolved and suspended solids,
which drained poorly. Martel and Vesilind79, subjecting samples of
wastewater sludges to variable rates of freezing and different final
temperatures, found that dewatering characteristics (as evaluated by
capillary suction time) showed the greatest improvement at the
slowest rate of freezing. (Although the final freezing temperature
also had an effect on dewatering characteristics, with lower tempera-
tures resulting in improved dewatering, the rate of freezing appeared
to be the significant factor.)
The direct-contact methods utilized in this study generally
resulted in rapid freezing, which appeared to promote cell rupture
and the production of fine particles, as evidenced by particle size
distribution data. The aggregation and densification noted as a
result of the indirect-contact process did not take place in the
direct-contact process.
The extent of freezing also differed between the direct-contact
and indirect-contact processes. In this study, the direct-contact
process was designed and conducted to produce approximately a slurry
composed of equal parts of ice and sludge, typical of the mixture
produced in salt water desalination. In comparison, sludges condi-
tioned with the indirect-contact process were allowed to freeze
solid. From the comparative results, it appears that the higher
fractions of ice formation (approaching a near total freeze) achieved
with the indirect-contact process may be necessary to achieve signif-
icant internal water removal and densification of sludge floc.
218
COMPARISON WITH OTHER STUDIES AND PROCESS VIABILITY
The purpose of this study was to develop a process model for
direct-contact, freeze-thaw processes within the existing context of
previous research and to gauge general process viability. The
following sections present comparisons of the results of this study
with earlier research and discuss the potential of future application
of direct-contact freeze-thaw conditioning processes.
Butane Conditioning
Selected results from research conducted by Khan30 to determine
the feasibility of conditioning waste activated sludge with butane in
a direct-contact process were previously presented in Table 1.
Khan3O observed substantial reductions in specific resistance and
large increases in dewatered solids concentration using high butane
doses (up to 1800 mL/L) in batch experiments and long contact times
(6 to 36 hours) in continuous experiments. Comparable results were
not obtained in the current study for waste activated sludge for any
freeze-thaw method, including the indirect-contact process. Several
factors may have contributed to this difference:
l. The dewatering characteristics of the unconditioned waste
activated sludge used in this study were far superior to
those of the unconditioned sludge used in Khan's study.
Typical specific resistance values for unconditioned waste 7
activated sludge in Khan's study ranged from 850 to 4700 x
219
1011 m/kg; in the current study, typical specific
resistance values for waste activated sludge ranged from 40
to 70 x 1011 m/kg. Therefore there was less room for
improvement in the current study.
2. Khan's best results from batch experiments were achieved at
butane doses that were at least 50 percent greater than
those used in this study. His best results from continuous
experiments were achieved at butane doses that were almost
twice as large as those used in this study and at very long
contact times. The extent of freezing achieved was likely
greater in Khan's study than in the current investigation,
and, in the continuous experiment, the rate of freezing
slower. Both of these factors would serve to improve
conditioning.
3. Khan limited mixing speeds to 45 rpm or less. This
moderate agitation probably minimized foaming, to which a
certain part of the deterioration of sludge quality
observed in this study has been attributed.
Freon Conditioning
Selected results from Molayem and Bardaki's33 feasibility study
utilizing Freon 11 to direct-contact freeze-thaw condition wastewater
Sludges were presented in Table 3. Large increases in final solids
220
were observed in certain experiments. As noted, however, Freon doses
were extremely large and results variable. Gains in solids
concentrations observed in the current study, while not as
substantial as the best results of Molayem and Bardaki's research,
were more consistent.
Process Viability
Although the results of the current study did not warrant
development of the experimental apparatus to larger scale or to
include refrigerant or heat recovery, several observations may be
made with respect to process viability:
1. External factors, e.g., mixing and reactor configuration,
appeared to have a significant effect on process results.
A viable process must include means of intimate contact
between sludge and refrigerant without disturbing floc
structure. In this study, mixing resulted in deteriorating
sludge quality by reducing particle size and exacerbating
refrigerant foaming. Possible alternative solutions exist,
such as higher refrigerant doses, application of sludge in
thin layers, and longer contact times; however, these
options tend to increase the cost of the operation and
reduce its potential for full-scale applications.w
221
2. Foaming is more likely to occur when back pressures in feed
systems cause partial volatilization30; but it also appears
to be depend upon the type of sludge. Since it is worst
for waste activated sludge, it may be enhanced by
biomass-produced surfactants.
3. Refrigerant hazards must be addressed. For example, butane
is both toxic and explosive; Freon 12 is toxic at high
concentrations and may become obsolete, as its potential as
an ozone-destroying agent is better defined.
4. Mechanical and operational complexity must be considered in
comparing direct-contact, freeze-thaw processes with other
alternatives. Temperature, pressure, mixing, and
refrigerant and sludge flowrates must be tightly
controlled. To be cost effective, the process must include
refrigerant and heat recovery, requiring sophisticated
compression and heat exchange systems.
5. Refrigerant and power costs are among the several
market-sensitive variables upon which the cost-
effectiveness of direct-contact, freeze—thaw processes
depend. The economic feasibility of these processes is
enhanced by market climates wherein energy costs are low.
222
VI. CONCLUSIONS
The results obtained in this study indicate that direct—contact,
freeze-thaw conditioning processes do not offer a panacea for
producing marked improvements in sludge dewatering properties. Long
conditioning times at slow rates of freezing may be necessary to
produce significant changes in floc size and water content,
parameters which ultimately affect the rate and extent of sludge
dewatering achieved. The rapid rate of freezing which characterized
the direct-contact conditioning investigated in this study produced
significant concentrations of fine particles, possibly as a result of
floc rupture. In contrast, the slow freezing of sludge to a solid,
as occurred in the indirect—contact process utilized in this study
(and as achieved by natural freezing colder climatic conditions)
resulted in the release of internal floc water and a corresponding
aggregation and densification of the floc structure, producing
excellent sludge dewatering characteristics.
The following specific conclusions were reached:
I. As evidenced by the results of the indirect-contact
process, freeze-thaw conditioning has the potential to
greatly increase dewatered solids concentration and reduce
specific resistance for both wastewater and water treatment
sludges.
223
2. The conditioning effects of freeze-thaw processes can be
explained by a two-stage model in which disruption of
sludge structure at the floc and particle level is followed
by formation of a new, denser floc structure.
3. Variability in the response of alum sludge, waste activated
sludge, primary sewage sludge, and mixtures of waste
activated and primary sewage sludges to freeze-thaw
conditioning can be attributed to inherent differences in
sludge characteristics. Freeze-thaw conditioning was most
effective in improving the dewatered solids concentration
of alum water treatment sludge.
4. The rapid and incomplete freezing characteristic of
direct-contact, freeze-thaw processes was not conducive to
significant changes in the particle and dewatering
characteristics of treated sludges.
5. The reduced performance of direct-contact, freeze-thaw
processes when compared to indirect-contact results may
also be attributed in part to the interfering effects of
mixing-induced changes in particle size distribution and of
refrigerant foaming.
224
Although significant improvements in dewatering characteristics
were not observed for sludge conditioned with direct-contact,
freeze-thaw processes, the results obtained in this study should not
necessarily be interpreted to show that future investigation of
direct-contact, freeze-thaw processes is unwarranted. Many other
agents form gas hydrates or clathrates with water; further testing is
appropriate with different compounds. The results of this study have
indicated which design parameters (e.g., rate of freezing, particle
properties) are critical to the potential success of such
conditioning methods.
225
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232
APPENDIX A
DESIGNATIONS FOR HALOGENATED HYDROCARBONS
Halogenated hydrocarbons used as secondary refrigerants share
the general formula °CaHbClCFd, where b+c+d = 2a + 2. Theserefrigerants are designated by a two- or three-digit number,
calculated from the variables above. The first digit equals (a-1),
unless this is zero, in which case, it is omitted. The second digit
equals (b+l), and the third, d.
If isomers occur, the most symmetrical is assigned the basic
designation, while "a" and successive lower case letters are appended
to isomers with decreasing symmetry. Brominated compounds are
designated by aui upper case B, followed by the number of bromine
atoms. The identifying number is preceded by either an F or an A
(indicating "Freon" or "Arcton") or by an R (for the general term
"Refrigerant"), or by the term for which the letter stands. For
example, monochlorodifluoroethane (CH3CClF2) is marketed as Freon
142b, where a = 2, b= 3, c = 1, d = 2, and a-1 = 1, b+1 = 4, d = 2,
and it is the third most symmetric isomer. It can be designated as
F-142b or R-142b.
[After Gosney, w. B., Principles of Refrigeration. Cambridge
University Press, New York, New York (1982).]
233
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