nchrp 24-31 lrfd design specifications for shallow ... on distribution of bridge foundation usage...
TRANSCRIPT
NCHRP Report 651
LRFD DESIGN AND CONSTRUCTION OF
SHALLOW FOUNDATIONS FOR HIGHWAY
STRUCTURES
Samuel G. Paikowsky, Mary C. Canniff, Kerstin Lesny,
Aloys Kisse, Shailendra Amatya, and Robert Muganga
Geosciences Testing & Research, Inc.
N. Chelmsford, MA USA
NCHRP 24-31 LRFD Design Specifications for Shallow
Foundations
TRB AFS30 Committee Meeting January 26, 2011
The lecture is based on
Geotechnical Engineering Research Laboratory
Dept. of Civil and Environmental Engineering
University of Massachusetts Lowell.
OBJECTIVES
NCHRP RESEARCH PROJECT 24-31
Develop and Calibrate Procedures and Modify AASHTO’s Section 10 (Foundations) Specifications for the Strength Limit State Design of Bridge Shallow Foundations.
For NCHRP Research Report 651, Google NCHRP 651
2
Task 1: Design & Construction Practices
Questionnaire - Establishing design methods,
construction practices, design cases, and loads
Developed and distributed to 161 State Highway
Officials, TRB Representatives, and State and
FHWA bridge engineers.
Obtained responses from 39 states and 1
Canadian Province
Previous relevant information was obtained via a
questionnaire circulated in 2004 for the research
project NCHRP 12-66 AASHTO LRFD
Specifications for the Serviceability in the Design
of Bridge Foundation
3
Design & Construction Practices - Questionnaire Foundation AlternativesResults on distribution of bridge foundation usage from our previous questionnaires conducted in 1999 and 2004, and the current questionnaire (over the past 3 years, 2004-2006):
shallow foundations driven piles drilled foundations
1999/2004 14%/17% 75%/62% 11%/21%
current 17% 59% 24%
The average use changes significantly across the country. The use of shallow foundations in the Northeast exceeds by far all other regions of the USA, ranging from 40% in NY, NJ and ME, to 67% in CT. Other “heavy users” are TN (63%), WA (30%), NV (25%) and ID (20%). In contrast, out of the 39 responding states, six states do not use shallow foundations for bridges at all, and additional eight states use shallow foundations in 5% or less of the highway bridge foundations.
In summary, 55.8% of the shallow foundations are built on rock(average of piers and abutments) with additional 16.8% on IGM, hence 72.6% of the foundations are build on rock or cemented soils and only 27.4% are built on soils of which 24.2% on granular soils and 3.2% on clay or silt.
4
TASK 2: DATABASES
UML-GTR ShalFound07 Database549 cases built in ACCESS platform, 415 cases are suitable for
ULS.
UML-GTR RockFound07 Capacity Database
122 Cases of load tests to failure including 61 rock sockets, 33
shallow foundations on rock surface, 28 shallow foundations
below surface
ShalFound07
Divided into vertical centric and eccentric, and inclined cases
RockFound07
All vertical centric, shallow and drilled shafts
5
Database – Overview
UML-GTR ShalFound07
Sand Gravel Cohesive Mix Others Germany Others
Plate load tests
B 1m346 46 -- 2 72 466 253 213
Small footings
1 < B 3m26 2 -- 4 1 33 -- 33
Large footings
3 < B 6m30 -- -- 1 -- 31 -- 31
Rafts & Mats
B > 6m13 -- -- 5 1 19 1 18
Total 415 48 0 12 74 549 254 295
Note:
“Mixed” are cases with alternating layers of sand or gravel and clay or silt
“Others” are cases with either unknown soil types or with other granular materials like loamy Scoria
1m 3.3ft
TotalPredominant Soil Type CountryFoundation
type
6
Large foundations are often not loaded to ULS failure (SLS controls)
TASK 3: BC Shallow Foundations on Soil - OUTLINE
1. BC of Shallow foundations
BC Factors
BC modification Factors
2. Determination of ULS from case histories ULS and Modes of Failure – Overview Modes of Failure
3. Failure (Ultimate Load) Criteria Minimum slope criteria (Vesić, 1963) Limited settlement criterion of 0.1B (Vesić, 1975) Log-log plot of load-settlement curve (DeBeer, 1967) Two-slope criterion Selection of failure criteria (representative values and minimum
slope) Examples in soil & rock
4. Uncertainty Evaluation – BC of Centric Vertically Loaded Footing on Granular Soils Database overview Calculated BC – missing soil parameters and equations used for BC
calculations
5. Calibration
6. Summary and Conclusions
7
Recommended Failure Criterion
Minimum Slope Failure Load Criterion, Vesic (1963)
Failure load interpreted were for 196 cases using each of the
proposed methods
“Representative Failure Load” defined as the mean value of all
the failure loads interpreted using each criterion
Mean of the ratio was 0.98 and
Failure Loads for most cases
could be interpreted using
Minimum Slope criterion – the
criterion was chosen as the
standard BC interpretation
method
8
Bias of Estimated BC
Cases with Vertical Centric Loading
Vertical Centric Loading
n = 173; mean bias = 1.59, COV = 0.291
Natural soil conditions
(f from SPT-N counts)
n = 14; no. of sites = 8
mean = 1.00
COV = 0.329
Controlled soil conditions
(Dr 35%)
n = 159; no. of sites = 7
mean = 1.64
COV = 0.267
B > 1.0m
n = 6
no. of sites = 3
mean = 1.01
COV = 0.228
0.1 < B 1.0m
n = 8
no. of sites = 7
mean = 0.99
COV = 0.407
B 0.1m
n = 138
no. of sites = 5
mean = 1.67
COV = 0.245
0.1 < B 1.0m
n = 21
no. of sites = 3
mean = 1.48
COV = 0.391
Figure 60 Summary of bias (measured over calculated BC) for vertical centric
loading cases (Database I); 0.1m = 3.94in; 1m = 3.28ft.
9
Bias of Estimated BC
Cases with Vertical Centric Loading
Figure 61. (a) Histogram and probability density functions of the bias and (b)
relationship between measured and calculated bearing capacity for all cases
of vertical centrically loaded shallow foundations.
0.2 0.6 1 1.4 1.8 2.2 2.6 3 3.4 3.8
Bias, qu,meas / qu,calc
0
10
20
30
40
Nu
mb
er o
f o
bse
rvat
ions
0
0.1
0.2
Fre
qu
ency
Vertical-centric loading
n = 173mean = 1.59
COV = 0.291
lognormal
distribution
normal
distribution
0.1 1 10 100Calcualted bearing capacity, qu,calc
(Vesic, 1975 and modified AASHTO)
(ksf)
0.1
1
10
100
Inte
rpre
ted
bea
ring c
apac
ity, q
u,m
eas
usi
ng
Min
imum
Slo
pe
crit
erio
n (
Ves
ic,
196
3)
(ksf
)
Vertical-centric loadingData (n = 173)
Data best fit line
No bias line
10
Bias of Estimated BC
Cases with Vertical Centric Loading
Figure 62. (a) Histogram and probability density functions of the bias and (b)
relationship between measured and calculated bearing capacity for vertical
centrically loaded shallow foundations on controlled soil conditions.
0.2 0.6 1 1.4 1.8 2.2 2.6 3 3.4 3.8
Bias, qu,meas / qu,calc
0
10
20
30
40
Nu
mb
er o
f o
bse
rvat
ions
0
0.1
0.2
0.3
Fre
qu
ency
Controlled soil conditions
n = 159mean = 1.64
COV = 0.267
lognormal
distribution
normal
distribution
0.1 1 10 100Calcualted bearing capacity, qu,calc
(Vesic, 1975 and modified AASHTO)
(ksf)
0.1
1
10
100
Inte
rpre
ted
bea
ring c
apac
ity, q
u,m
eas
usi
ng
Min
imum
Slo
pe
crit
erio
n (
Ves
ic,
196
3)
(ksf
)
Controlled soil conditionsData (n = 159)
Data best fit line
No bias line
11
Bias of Estimated BC
Cases with Vertical Centric Loading
Figure 63. (a) Histogram and probability density functions of the bias and (b)
relationship between measured and calculated bearing capacity for vertical
centrically loaded shallow foundations on natural soil conditions.
0.2 0.6 1 1.4 1.8 2.2 2.6 3 3.4 3.8
Bias, qu,meas / qu,calc
0
1
2
3
4
5
6
Nu
mb
er o
f o
bse
rvat
ions
0
0.1
0.2
0.3
0.4
Fre
qu
ency
Natural soil conditions
n = 14
mean = 1.00
COV = 0.329
lognormal
distribution
normal
distribution
1 10 100Calcualted bearing capacity, qu,calc
(Vesic, 1975 and modified AASHTO)
(ksf)
1
10
100
Inte
rpre
ted
bea
ring c
apac
ity, q
u,m
eas
usi
ng
Min
imum
Slo
pe
crit
erio
n (
Ves
ic,
196
3)
(ksf
)
Natural soil conditionsData (n = 14)
Data best fit line
No bias line
12
Bias versus Footing Width
Figure 100. Variation of the bias in bearing resistance versus footing
size for cases under vertical-centric loadings: f 43 and f < 43.
0.01 0.1 1
Footing width, B (m)
0.5
1
1.5
2
2.5
3
3.5
Bia
s
0.1 1 10B (ft)
(5)
(34)
(4)
(90)
(5)
(2)
(1)(17)
(1)
(3)
(4)
(3)
(1)
(2)
Mean bias BC (n = 172) s.d.
(x) no. of cases in each interval
95% confidence interval for f (n = 135)
95% confidence interval for f (n = 37)
13
Uncertainty in N
Comparison of bearing capacity factor calculated based on test results;
N = qu / (0.5 B s) from 125 tests carried out in controlled soil conditions
(tests by Perau, 1995) and N proposed by Vesic (1973) in the range of soil
friction angle of 42 and 46
42 43 44 45 46
friction angle, f (deg)
10
100
1000q
u /
(0.5
B
s)
N from load tests; n = 125
N (Vesic, 1973)
N = exp(0.39f 11.546)
(R2 = 0.666)
14
Uncertainty in N
42 43 44 45 46
Friction Angle, f (deg)
0
0.5
1
1.5
2
2.5
3
N
= [
qu /
(0.5
B
s)
] /
NV
esic
load test data; n = 125
= exp(0.205f 8.655) (R2 = 0.351)
Figure 93. The ratio (N) between the back-calculated B.C. factor N
based on experimental data to that proposed by Vesić versus soil
friction angle.
15
Uncertainty in N
Figure 94. The ratio between measured and calculated bearing
capacity (bias ) compared to the bias in the B.C. factor N (N) versus
the soil’s friction angle for footings under vertical-centric loadings.
43 44 45 46
Friction Angle, f (deg)
0
0.5
1
1.5
2
2.5
3
Bia
s
Data BC bias (n = 131)
Bearing Capacity (BC) bias,
N bias,
16
Uncertainty in B.C.
Figure 103. Bearing resistance bias vs. average soil friction angle
(taken f 0.5) including 95% confidence interval for all cases under
vertical-centric loading.
30 32 34 36 38 40 42 44 46
Friction angle f (deg)
0.0
0.5
1.0
1.5
2.0
2.5
3.0
3.5
Bia
s
(2)
(90)
(30)
(14)(4)
(2)
(12)
(4)
(3)
(2)
(3)
(4)
(2)
Mean bias,BC (n = 172) 1 s.d.
(x) no. of cases in each interval
BC = 0.308exp(0.0372f)
(R2=0.200)
95% confidence interval
17
Final Resistance Factors – Controlled Conditions
Table 66 Recommended resistance factors for shallow foundations on granular
soils placed under controlled conditions
Soil friction
angle f
Loading conditions
Vertical-centric or
-eccentricInclined-centric
Inclined-eccentric
Positive Negative
0° ° 0.500.40 0.40 0.70
° ° 0.60
° 9° 0.70 0.45 0.45 0.75
0° ° 0.75 0.500.50 0.80
° 0.80 0.55
Notes:
1) f determined by laboratory testing
2) compacted controlled fill or improved ground are assumed to extend below the base
of the footing to a distance to at least two (2.0) times the width of the foundation (B).
If the fill is less than 2B thick, but overlays a material equal or better in strength than
the fill itself, then the recommendation stands. If not, then the strength of the
weaker material within a distance of 2B below the footing; prevails.
3) The resistance factors were evaluated for a target reliability T = 3.0.
18
Final Resistance Factors – Natural Conditions
Table 67 Recommended resistance factors for shallow foundations on natural
deposited granular soil conditions
Notes:
1) f determined from Standard Penetration Test results
2) granular material is assumed to extend below the base of the footing at least two
(2.0) times the width of the foundation.
3) The resistance factors were evaluated for a target reliability T = 3.0
Soil friction
angle f
Loading conditions
Vertical-centric or
-eccentricInclined-centric
Inclined-eccentric
Positive Negative
0° ° 0.400.40
0.35 0.65
° ° 0.450.70
° 9° 0.500.40
0° ° 0.55 0.450.75
° 0.65 0.50 0.45
19
Intermediate Conclusions and Summary
It was found that for the footings of larger sizes (B>3m (9.9ft)),
the load tests were not carried out to the failure load
Biases for the tests in Natural Soil Condition and Controlled
Soil Conditions were analyzed separately
For the footing sizes in similar ranges (0.1m < B 1.0m), the
scatter of bias was larger for footings on/in natural soil
conditions
The majority of the relevant data refers to small size
foundations (B 3.3ft (1.0m)) on controlled compacted
material. Many of the highway shallow foundations on soils
are built on compacted materials and hence, the statistical
data of the uncertainty can be used for that purpose
There appears to be a trend of increase in bias with the
footing size within the range of footing sizes available for
testing (which seems to conform with the observation made
by Vesic (1969))
20
ULS of Inclined Loading
Figure 64. Loading convention and load paths used during
tests.
3b
1x
2F3M
1M
2M1F
2x
3F
2b
D
3x
g
f
B
1x
2F 3M
1M 2M1F
2x
3F
L
D
3x
(a) Loading convention
F1
F3
F1
F3
1,const.
increasing = const.
F1
M2
arctan e = const
(b) Radial load path (c) Step-like load path
F
Figure 4.7. Loading convention and load paths used during tests
21
ULS of Inclined Loading
Figure 65. Load–displacements curves for model tests
conducted by Montrasio (1994) with varying load inclination:
(a) vertical load vs. vertical displacement and (b) horizontal
load vs. horizontal displacement.
0 1 2 3 4
Vertical load, F1 , F10 (kN)
8
6
4
2
0
Ver
tica
l d
ispla
cem
ent, u
1 (
mm
)
0 0.2 0.4 0.6 0.8 1F1 (kips)
0.3
0.2
0.1
0
u1 (
in)
MoD2.1 = 3
MoD2.2 = 8
MoD2.3 = 14
MoA2.1 = 0F0
0 0.2 0.4 0.6 0.8 1 1.2
Horizontal load, F3 (kN)
6
4
2
0
Ho
rizo
nta
l d
ispla
cem
ent, u
3 (
mm
)0 0.05 0.1 0.15 0.2 0.25
F3 (kips)
0.2
0.1
0
u3 (
in)
MoD2.1 = 3
MoD2.2 = 8
MoD2.3 = 14
22
Figure 66. (a) Histogram and probability density functions of
the bias and (b) relationship between measured and calculated
bearing capacity for all cases of vertical eccentrically loaded
shallow foundations.
0.4 1.2 2 2.8 3.6
Bias, qu,meas / qu,calc
0
2
4
6
8
10
12
Nu
mb
er o
f o
bse
rvat
ions
0
0.05
0.1
0.15
0.2
0.25
Fre
qu
ency
Vertical-eccentric loading
n = 43mean = 1.83
COV = 0.351
lognormal
distribution
normal
distribution
0.1 1 10 100Calcualted bearing capacity, qu,calc
(Vesic, 1975 and modified AASHTO)
(ksf)
0.1
1
10
100
1000
Inte
rpre
ted
bea
ring c
apac
ity, q
u,m
eas
usi
ng
Min
imum
Slo
pe
crit
erio
n (
Ves
ic,
196
3)
(ksf
)
Vertical-eccentric loadingData (n = 43)
Data best fit line
No bias line
Bias of Estimated BC
Cases with Vertical-Eccentric Loading (using B)
23
Figure 105. Bearing resistance bias versus soil friction angle for
cases under vertical-eccentric loadings; seven cases for f = 35
(all from a single site) have been ignored for obtaining the
best fit line.
30 32 34 36 38 40 42 44 46
Friction angle f (deg)
0.0
0.5
1.0
1.5
2.0
2.5
3.0
Bia
s
(7)
(6)
(4)
(2)
(9)
(4)
(11)
Mean bias, BC 1 s.d.
(x) no. of cases in each interval
BC = 2.592´exp(-0.01124f) (R2=0.01)
95% confidence interval
n = 43
Bias of Estimated BC
Cases with Vertical-Eccentric Loading
24
Figure 67. (a) Histogram and probability density functions of the
bias and (b) relationship between measured and calculated
bearing capacity for all cases of inclined centric loaded shallow
foundations.
0.2 0.6 1 1.4 1.8 2.2 2.6
Bias, qu,meas / qu,calc
0
4
8
12
Nu
mb
er o
f o
bse
rvat
ions
0
0.1
0.2
0.3
Fre
qu
ency
Inclined-centric loading
n = 39
mean = 1.43
COV = 0.295
lognormal
distributionnormal
distribution
0.1 1 10 100Calcualted bearing capacity, qu,calc
(Vesic, 1975 and modified AASHTO)
(ksf)
0.1
1
10
100
Inte
rpre
ted
bea
ring c
apac
ity, q
u,m
eas
usi
ng
Min
imum
Slo
pe
crit
erio
n (
Ves
ic,
196
3)
(ksf
)
Inclined-centric loadingData (n = 39)
Data best fit line
No bias line
Bias of Estimated BC
Cases with Inclined-Centric Loading
25
Figure 68. (a) Histogram and probability density functions of the
bias and (b) relationship between measured and calculated
bearing capacity for all cases of inclined eccentrically loaded
shallow foundations.
1.2 1.8 2.4 3 3.6 4.2 4.8 5.4 6 6.6 7.2
Bias, qu,meas / qu,calc
0
1
2
3
4
5
6
7
8
9
Nu
mb
er o
f o
bse
rvat
ions
0
0.05
0.1
0.15
0.2
0.25
0.3
Fre
qu
ency
Inclined-eccentric loading
n = 29
mean = 2.43
COV = 0.508
lognormal
distribution
normal
distribution
0.1 1 10 100Calcualted bearing capacity, qu,calc
(Vesic, 1975 and modified AASHTO)
(ksf)
0.1
1
10
100
Inte
rpre
ted
bea
ring c
apac
ity, q
u,m
eas
usi
ng
Min
imum
Slo
pe
crit
erio
n (
Ves
ic,
196
3)
(ksf
)
Inclined-eccentric loadingData (n = 29)
Data best fit line
No bias line
Bias of Estimated BC
Cases with Inclined-Eccentric Loading
26
Loading Directions for Inclined-Eccentric Loadings
Figure 69. Loading directions for the case of inclined-eccentric
loadings: (a) along footing width and (b) along footing length
e
3
F
1
b
3
F
3
M2
F
1 F
3
+
+
e
3
F
1
b
3
F
3
M2
F
1 F
3
+
Moment acting in the same direction as the lateral loading – positive
eccentricity
Moment acting in direction opposite to the lateral loading – negative
eccentricity
b
3
b
3
(a) along footing width
e
2
F
1
b
2
F
2
M3
F
1
b
2
F
2
+
-
e
2
F
1
b
2
F
2
M3
F
1
b
2
F
2
+
+
Moment acting in the same direction as the lateral loading – positive
eccentricity
Moment acting in direction opposite to the lateral loading – negative
eccentricity
(b) along footing length
27
Figure 71. (a) Histogram and probability density functions of the
bias and (b) relationship between measured and calculated
bearing capacity for all cases of inclined eccentrically loaded
shallow foundations under negative eccentricity.
1.2 1.8 2.4 3 3.6 4.2 4.8 5.4 6 6.6 7.2
Bias, qu,meas / qu,calc
0
1
2
3
Nu
mb
er o
f o
bse
rvat
ions
0
0.1
0.2
0.3
0.4
0.5
Fre
qu
ency
Inclined-eccentric loading
Negative eccentricity
n = 7
mean = 3.43
COV = 0.523
normal
distribution
lognormal
distribution
0.1 1 10Calcualted bearing capacity, qu,calc
(Vesic, 1975 and modified AASHTO)
(ksf)
0.1
1
10
Inte
rpre
ted
bea
ring c
apac
ity, q
u,m
eas
usi
ng
Min
imum
Slo
pe
crit
erio
n (
Ves
ic,
196
3)
(ksf
)
Inclined-eccentric loading
Negative eccentricityData (n = 7)
Data best fit line
No bias line
Bias of Estimated BC
Cases with Inclined-Eccentric Loading
28
Final Resistance Factors – Natural Conditions
Table 67 Recommended resistance factors for shallow foundations on natural
deposited granular soil conditions
Notes:
1) f determined from Standard Penetration Test results
2) granular material is assumed to extend below the base of the footing at least two
(2.0) times the width of the foundation.
3) The resistance factors were evaluated for a target reliability T = 3.0
Soil friction
angle f
Loading conditions
Vertical-centric or
-eccentricInclined-centric
Inclined-eccentric
Positive Negative
0° ° 0.400.40
0.35 0.65
° ° 0.450.70
° 9° 0.500.40
0° ° 0.55 0.450.75
° 0.65 0.50 0.45
29
Developed as a part of Project NCHRP 12-66
Bias = measured load / calculated load for a given
settlement
For reliability index = 1.28 (pf = 10%), and load
factors taken as unity
Bias of LL = 1.15, COVQL = 0.2
Bias of DL = 1.05, COVQD = 0.1
Method Range of Settlement
(inch)
Resistance Factor
Efficiency Factor
/
0.00 < 1.00 0.85 0.34
1.00 < 1.50 0.80 0.48 AASHTO
1.50 < 3.00 0.60 0.48
Conceptual Design – Influence of Serviceability
’s based on Serviceability Limit States
30
Conceptual Design – Granular Soils
Example 2 NCHRP Report 651: Known Load and
Settlement
Central Pier of a
bridge in Billerica
(Rangeway Rd over
Rte.3) (B-12-025)
Design (factored)
load is 3688.3kips
for ultimate limit
state and 2750kips
for service limit state
(unfactored)
Allowable settlement
1.5inches
31
Conceptual Design – Granular Soils
Factored Resistances (ksf)
32
2 4 6 8 10 12 14 16 18 20 22
Effective footing width, B (ft)
0
1000
2000
3000
4000
5000
Fac
tore
d u
ltim
ate
lim
it s
tate
an
d
unfa
ctore
d s
ervic
e li
mit
sta
te (
kip
s)
1 2 3 4 5 6
Effective footing width, B (m)
0
5
10
15
20
Fac
tore
d u
ltim
ate
lim
it s
tate
an
d
un
fact
ore
d s
ervic
e li
mit
sta
te (
MN
)
2 4 6 8 10 12 14 16 18 20 22
Effective footing width, B (ft)
0
5
10
15
20
25
Fac
tore
d u
ltim
ate
lim
it s
tate
an
d
unfa
ctore
d s
ervic
e li
mit
sta
te (
ksf
)
1 2 3 4 5 6
Effective footing width, B (m)
0
0.25
0.5
0.75
1
Fac
tore
d u
ltim
ate
lim
it s
tate
an
d
un
fact
ore
d s
erv
ice
lim
it s
tate
(M
Pa)
Strength LS, C2 load 00
Strength LS, C7 load 0
Strength LS 0AASHTO, 2007)
Service LS AASHTO (2007)
Service LS Schmertmann (1978)
Service LS Hough (1959)
Service I loading
Strength I, C2 loading
Strength I, C7 loading2 4 6 8 10 12 14 16 18 20 22
Effective footing width, B (ft)
0
1000
2000
3000
4000
5000
Fac
tore
d u
ltim
ate
lim
it s
tate
an
d
unfa
ctore
d s
ervic
e li
mit
sta
te (
kip
s)
1 2 3 4 5 6
Effective footing width, B (m)
0
5
10
15
20
Fac
tore
d u
ltim
ate
lim
it s
tate
an
d
un
fact
ore
d s
ervic
e li
mit
sta
te (
MN
)
2 4 6 8 10 12 14 16 18 20 22
Effective footing width, B (ft)
0
5
10
15
20
25
Fac
tore
d u
ltim
ate
lim
it s
tate
an
d
unfa
ctore
d s
ervic
e li
mit
sta
te (
ksf
)
1 2 3 4 5 6
Effective footing width, B (m)
0
0.25
0.5
0.75
1
Fac
tore
d u
ltim
ate
lim
it s
tate
an
d
un
fact
ore
d s
erv
ice
lim
it s
tate
(M
Pa)
Strength LS, C2 load 00
Strength LS, C7 load 0
Strength LS 0AASHTO, 2007)
Service LS AASHTO (2007)
Service LS Schmertmann (1978)
Service LS Hough (1959)
Service I loading
Strength I, C2 loading
Strength I, C7 loading
Figure H-6 Variation of factored bearing resistance for Strength-I and
unfactored resistance for Service-I limit state with effective footing width for
Example 2 (NCHRP Report 651)
Conceptual Design – Granular Soils
Factored Resistances (kips)
Strength Limit State
loading
3688kips (phi=0.45)
B = 8.9ft (B’=7.9ft+2x0.5)
Service Limit state of
2750kips – B=4.5ft
(B’=3.5+2x0.5)
33
2 4 6 8 10 12 14 16 18 20 22
Effective footing width, B (ft)
0
1000
2000
3000
4000
5000
Fac
tore
d u
ltim
ate
lim
it s
tate
an
d
unfa
ctore
d s
ervic
e li
mit
sta
te (
kip
s)
1 2 3 4 5 6
Effective footing width, B (m)
0
5
10
15
20
Fac
tore
d u
ltim
ate
lim
it s
tate
an
d
un
fact
ore
d s
ervic
e li
mit
sta
te (
MN
)
2 4 6 8 10 12 14 16 18 20 22
Effective footing width, B (ft)
0
5
10
15
20
25
Fac
tore
d u
ltim
ate
lim
it s
tate
an
d
unfa
ctore
d s
ervic
e li
mit
sta
te (
ksf
)
1 2 3 4 5 6
Effective footing width, B (m)
0
0.25
0.5
0.75
1
Fac
tore
d u
ltim
ate
lim
it s
tate
an
d
un
fact
ore
d s
erv
ice
lim
it s
tate
(M
Pa)
Strength LS, C2 load 00
Strength LS, C7 load 0
Strength LS 0AASHTO, 2007)
Service LS AASHTO (2007)
Service LS Schmertmann (1978)
Service LS Hough (1959)
Service I loading
Strength I, C2 loading
Strength I, C7 loading
Figure H-6 cont. Variation of factored bearing resistance for Strength-I and
unfactored resistance for Service-I limit state with effective footing width for
Example 2 (NCHRP Report 651)
2 4 6 8 10 12 14 16 18 20 22
Effective footing width, B (ft)
0
1000
2000
3000
4000
5000
Fac
tore
d u
ltim
ate
lim
it s
tate
an
d
unfa
ctore
d s
ervic
e li
mit
sta
te (
kip
s)
1 2 3 4 5 6
Effective footing width, B (m)
0
5
10
15
20
Fac
tore
d u
ltim
ate
lim
it s
tate
an
d
un
fact
ore
d s
ervic
e li
mit
sta
te (
MN
)
2 4 6 8 10 12 14 16 18 20 22
Effective footing width, B (ft)
0
5
10
15
20
25
Fac
tore
d u
ltim
ate
lim
it s
tate
an
d
unfa
ctore
d s
ervic
e li
mit
sta
te (
ksf
)
1 2 3 4 5 6
Effective footing width, B (m)
0
0.25
0.5
0.75
1
Fac
tore
d u
ltim
ate
lim
it s
tate
an
d
un
fact
ore
d s
erv
ice
lim
it s
tate
(M
Pa)
Strength LS, C2 load 00
Strength LS, C7 load 0
Strength LS 0AASHTO, 2007)
Service LS AASHTO (2007)
Service LS Schmertmann (1978)
Service LS Hough (1959)
Service I loading
Strength I, C2 loading
Strength I, C7 loading
Intermediate Conclusions
The Strength Limit State governs the footing
dimensions in this design example with a
requirement for B=8.9ft vs. B=4.5ft for the service
limit state
The bridge was designed with B=13.1ft most likely
due to the differences in design procedures
(especially settlement)
34
Task 3: BC Shallow Foundations on Rock - OUTLINE
1. Broad Objectives
2. Database UML/GTR RockFound07
3. Rock Classification and Properties
4. Methods of Analyses Selected for
Establishing the Uncertainty in B.C. of
Foundations on Rock
5. Calibration – evaluation of resistance
factors
6. Summary and Conclusions
35
2. DATABASE UML/GTR RockFound 07
Comprised of 122 foundation case histories of load tests in/on rock and IGM’s.
The database has 61 footings cases (28 cases D>0, 33 cases D=0) and 61 rock socket cases for which the base behavior (load and displacement) under loading was monitored.
89 of the 122 cases were used for the uncertainty determination of the settlement of foundations on rock.
36
Hirany and Kulhawy (1988)
proposed the L1-L2 method
for interpreting the "failure"
load or "ultimate" capacity
of foundations from load-
displacement curves.
Hirany and Kulhawy (1988) Failure criterion
The unique peak or
asymptote value in the
curves is taken as the
measured or interpreted
capacity (QL2=qL2).
For 79 cases qL2 could be
evaluated, 43 cases are
based on reported failure
load.
37
Using the limit-equilibrium approach, Carter and
Kulhawy (1988) developed a lower bound to the B.C. for
strip and circular footings on jointed rock masses
presented below.
uult qsmq (2)
Carter and Kulhawy (1988) - B.C. of Foundations on Rock
38
Relationship between Carter and Kulhawy (1988) calculated bearing
capacity (qult) using two variations (equations 82a and 82b) and the
interpreted bearing capacity (qL2).
Carter and Kulhawy (1988) - B.C. of Foundations on Rock
39
0.01 0.1 1 10 100 1000 10000 100000
Carter and Kulhawy (1988) Bearing Capacity qult (ksf)
1
10
100
1000
10000
100000
Inte
rpret
ed F
ou
nd
ati
on
Cap
aci
ty q
L2 (
ksf
)
58 Footings cases
61 Rock Socket cases
119 All cases withrevised equation
qL2 = 16.14 qult)0.619
(n = 119; R2 = 0.921)
qL2 = 36.51 qult)0.600 (Revised)
(n = 119; R2 = 0.917)
qL2 = qult
Table 69 Calibrated resistance factors for different datasets of resistance bias
obtained using Carter and Kulhawy’s (1988) method
Carter and Kulhawy (1988) - B.C. of Foundations on Rock
40
Dataset No. of casesBias Resistance factor (T = 3)
Mean COV MCS Recommended
All cases 119 8.00 1.240 0.372 0.35
RMR 85 23 2.93 0.651 0.535 0.50
65 RMR < 85 57 3.78 0.463 1.149 1.00
44 RMR < 65 17 8.83 0.651 1.612 1.00
3 RMR < 44 22 23.62 0.574 5.295 1.00
The lower bound is represented by the following Equation:
1Nqquult
2
45tanN 2
in which
Goodman (1989) developed the B.C.
Equation 5 for footings resting on
orthogonal vertical joints each
spaced distance s in which lateral
stress transfer is nil.
1B
SN
1N
1qq
N1N
uult
(3)
(4)
(5)
Goodman (1989) - B.C. of Foundations on Rock
41
Summary of the statistics for the Ratio of Measured to Calculated
B.C. using Goodman’s (1989) Method
Cases nNo. of
Sites
Mean of
Bias
m
Standard
Deviation
s
COV
All Foundations 119 78 1.35 0.72 0.535
All rock sockets 61 49 1.52 0.82 0.541
All footings 58 29 1.23 0.66 0.539
Sub-categorization suggests that if more details of rock
measurements are available, the uncertainty is reduced.
1. 34 Rock Socket cases with measured discontinuity
spacing had a COVl = 0.48.
2. 8 Rock Socket cases with measured discontinuity
spacing and friction angle had a COVl = 0.18.
Goodman (1989) - B.C. of Foundations on Rock
42
Figure 78. Relationship between Goodman’s (1989) calculated bearing capacity
(qult) and the interpreted bearing capacity (qL2).
Goodman (1989) - B.C. of Foundations on Rock
43
1 10 100 1000 10000 100000
Goodman (1989) Bearing Capacity qult (ksf)
1
10
100
1000
10000
100000
Inte
rpret
ed
Fou
nd
ati
on
Cap
acit
y q
L2 (
ksf
)
58 Footings cases
61 Rock Socket cases
qL2 = 2.16 qult)0.868
(n = 119; R2 = 0.897)
qL2 = qult
Goodman (1989) - B.C. of Foundations on Rock
44
0 0.6 1.2 1.8 2.4 3 3.6 4.2 4.8
Bias, qu,meas / qu,calc
0
10
20
30
40
Nu
mb
er
of
observ
ati
ons
0
0.05
0.1
0.15
0.2
0.25
0.3
0.35
Fre
qu
ency
119 Rock-sockets and Footing cases
Goodman (1989)
mean = 1.35
COV = 0.535
lognormal
distribution
normal
distribution
0 0.4 0.8 1.2 1.6 2 2.4 2.8 3.2
Bias, qu,meas / qu,calc
0
2
4
6
8
10
12
Nu
mb
er o
f o
bse
rvat
ions
0
0.1
0.2
0.3
0.4
0.5
0.6
Fre
qu
ency
20 Foundation cases on Fractured Rocks
Goodman (1989)
mean = 1.24
COV = 0.276
lognormal
distribution
normal
distribution
Figure 79. Distribution of the ratio of the
interpreted bearing capacity (qL2) to the
bearing capacity (qult) calculated using
Goodman’s (1989) method for the rock
sockets and footings in database UML-GTR
RockFound07.
Figure 80. Distribution of the ratio of the
interpreted bearing capacity (qL2) to the
bearing capacity (qult) calculated using
Goodman’s (1989) method for foundations
on fractured rock in database UML-GTR
RockFound07
Goodman (1989) - B.C. of Foundations on Rock
45
-4
-2
0
2
4
Sta
nd
ard
norm
al
qu
an
tile
0.0 0.5 1.0 1.5 2.0 2.5 3.0 3.5 4.0 4.5
Bias
B.C. using Goodman (1989)All data
Total data (n = 119)
Normal distribution
Lognormal distribution
= 1.35
COV = 0.535
Figure 113. Comparison of the unfiltered bias for BC calculated using Goodman
(1989) method for all data and the theoretical normal and lognormal distributions.
Table 68 Calibrated resistance factors for different datasets of resistance
bias obtained using Goodman’s (1989) method
Goodman (1989) - B.C. of Foundations on Rock
46
Dataset No. of casesBias Resistance factor (T = 3)
Mean COV MCS Recommended
All data 119 1.35 0.535 0.336 0.30
Measured friction angle f 98 1.41 0.541 0.346 0.35
Measured spacing s 83 1.43 0.461 0.437 0.40
Measured friction angle f and s 67 1.51 0.459 0.464 0.45
Calibration of Resistance Factors
47
Method of
AnalysisEquation Application
Efficiency Factor
/
(%)
Carter and
Kulhawy
(1988)
All 0.35 4.4
RMR 85 0.50 17.1
65 RMR < 85
1.00
26.5
44 RMR < 65 11.3
3 RMR < 44 4.2
Goodman
(1989)
For fractured rocks:
For non-fractured rocks:
All 0.30 22.2
Measured f 0.35 24.8
Measured s 0.40 28.0
Measured s and f 0.45 29.8
ult uq q m s
1ult uq q N
( 1)1
11
N N
ult u
sq q N
N B
Table 70 Recommended resistance factors for foundations in/on
rock based on T = 3.0 (pf = 0.135%)
Uncertainty in B.C.
Figure 104. Recommended resistance factors for soil friction angles (taken f 0.5) between 30 and
46, with comparisons to 95% confidence interval and resistance factors obtained for the cases in the
database; the bubble size represents the number of data cases in each subset.
30 32 34 36 38 40 42 44 46
Friction angle f (deg)
0.0
0.2
0.4
0.6
0.8
1.0
Res
ista
nce
fact
or,
0.0
0.5
1.0
1.5
2.0
2.5
3.0
Bia
s
(2)(90)
(30)
(14)(4)
(2)
(12)
(4)
(3)
(2)(3)
(4)
(2)
95% confidence interval for
Resistance factor based on database(x) no. of cases in each interval
Recommended f for Controlled soil conditions
Recommended f for Natural soil conditions
n = 172
49
Table 38 Summary of the statistics for the ratio of measured (qL2) to calculated
bearing capacity (qult) of rock sockets and footings on rock using Carter and
Kulhawy (1988) method
Carter and Kulhawy (1988) - B.C. of Foundations on Rock
50
Cases nNo. of
Sitesm s COV
All rock sockets 61 49 4.29 3.08 0.716
All rock sockets on fractured rock 11 6 5.26 1.54 0.294
All rock sockets on non-fractured rock 50 43 4.08 3.29 0.807
Rock sockets on non-fractured rock with measured discontinuity
spacing (s')34 14 3.95 3.75 0.949
Rock sockets on non-fractured rock with s' based on AASHTO
(2007)16 13 4.36 2.09 0.480
All footings 58 29 11.90 12.794 1.075
All footings on fractured rock 9 3 2.58 2.54 0.985
All footings on non-fractured rock 49 26 13.62 13.19 0.969
Footings on non-fractured rock with measured discontinuity
spacing (s')29 11 15.55 14.08 0.905
Footings on non-fractured rock with s' based on AASHTO
(2007)20 11 10.81 11.56 1.069
n = number of case histories m = mean of biases s = standard deviation
COV = coefficient of variation Calculated capacity based on equation (82a)
Table 40 Summary of the statistics for the ratio of measured (qL2) to
calculated bearing capacity (qult) of rock sockets and footings on rock
using Goodman (1989) method
Goodman (1989) - B.C. of Foundations on Rock
51
Cases nNo. of
Sitesm s COV
All 119 78 1.35 0.72 0.535
Measured discontinuity spacing (s') and friction angle (f) 67 43 1.51 0.69 0.459
Measured discontinuity spacing (s') 83 48 1.43 0.66 0.461
Measured friction angle (f) 98 71 1.41 0.76 0.541
Fractured 20 9 1.24 0.34 0.276
Fractured with measured friction angle (f) 12 7 1.33 0.25 0.189
Non-fractured 99 60 1.37 0.77 0.565
Non-fractured with measured s' and measured f 55 37 1.55 0.75 0.485
Non-fractured with measured discontinuity spacing (s') 63 39 1.49 0.72 0.485
Non-fractured with measured friction angle (f) 86 64 1.42 0.81 0.569
Spacing s' and f, both based on AASHTO (2007) 5 3 0.89 0.33 0.368
Discontinuity spacing (s') based on AASHTO (2007) 36 21 1.16 0.83 0.712
Friction angle (f) based on AASHTO (2007) 21 7 1.06 0.37 0.346n = number of case histories m = mean of biases s = standard deviation COV = coefficient of
variation