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Section 4 . ~ ) . : 3 presents evidence that K
2
b is likely to be
around 2.0, not LO. On the other hand, the calculated
stresses are based on intersecting shells with no fillet
weld or radius. These stresses attenuate very rapidly,
sometimes by 50% within one wall thickness. In fatigue
test models, the fillet weld or outer fillet radius may
cover this high stressed area, and thereby significantly
reduce the
actual
stresses as compared with the calcu
lated stresses. Further, the fillet weld or outer radius
may provide reinforcement in the critical intersection
zone.
In
the sense
that
protection against fatigue
is
the
rationale behind
the
Code evaluat ions using i-factors,
we view
the
fatigue test s as more directly relevant
than
calculated stresses. We
thus
view
Table 15
compari
sons as
an
adequate basis for the proposed
i
for
RIT
up
to about
25. (Note
that the
maximum
R/T
in
Table
14
is 18.2.)
Based
on all present evidence, we
think
it is
reasonably valid for R/T up to 50.
As
a final
point,
note
that
i
covers the full range
of
r/R;
hence,
the
UFT can be deleted from Fig. NC-
3673.2(b)-1.
Indeed, if
it
is
not deleted, the underesti
mate of
i
for Mob would
remain
in the Code.
6.0 References
1. Mark , A. R. C. and George, H. H.,
"Fatigue
Tests on Flanged Assemb·
Trans ASME,
82,77-87, (19 )0).
Mark ,
A. R.
C.
"Fatigue Tests
of
Piping
Components,"
Trans. ASME,
74,287-303, (1952).
3. ANSI
B3Ll,
"Power
Piping,"
1983 Edition, ASME, New York.
4.
ANSI B31.3, "Chemical
Plant
and
Petroleum
Refinery Piping," 1983
Edition, ASME,
New
York.
5. ASME
Boiler and
Pressure
Vessel Code, Section
Ill.
Division l.
"Nucle
ar
Power
Plant Components," 1983 Ed. with Winter 1984 Addenda, New
York, NY 10017.
6. Blair,
J.
S.,
"Heinforcment of Branch
Pieces,"
Engineering,
London,
England, 1947.
7. Pickett, A.
G.,
et al.,
"Low
Cycle Fatigue Testing
of
One-Half Scale
Model
Pressure
Vessels," Progress
Reports
No. 9-12.
Southwest
Research
Institute, San Antonio,
Texas, July 1964-.Jan. 1965.
8. Decock,
J.,
"External
Loadings
on Nozzles in Cylindrical Shells.'' 4th
lnt'L
Conf.
on Press.
Vessel Technology, J. Mech. Eng., 1980.
9. Davies, J. B. and
Jaske.
C. E. "Fatigue Evaluation of Weldolet Branch
Connections
in
Carbon Steel Pipe," Battelle-Columbus Report
to
Bonney
Forge, Allentown, PA 18105, Aug. 30, 1974.
10.
Tableriou,
J .P . and Walsh, D .,
"Determination of
Stress Intensifica
tion
Factors
for
the
Code
Qualification
of Integrally Reinforced
Branch
Con
nections," ASME Paper No.
78-PVP-66
and "Final
Report
on 1979 S F
Testing Program.''
Target
Technology Report
to WFL Inc.,
Houston, Texas
77008, Aug. 22, 1979.
11.
Forte, T. P.,
"Fatigue
Evaluation
of 6 x 4 Weldolet Branch
Connections
in
Carbon
Steel Pipe," Battelle-Columbus Report to Bonney Forge, Allen
town,
PA
18105, Dec. 31, 1981.
12. Davies, K.
B.
and
Jaske,
C. E.,
"Fatigue
Evaluation
of
12 x 6
Weldolet
Branch Connections
in
Carbon
Steel
Pipe,"
Battelle-Columbus
Report
to
Bonney Forge, Allentown, PA 18105, June 25, 1975.
13.
Forte, T. and
.Jaske, C. E.
"Fatigue
Evaluation of
14 x
6lnsert
Weldolet
Branch Connections
in
Carbon
Steel
Pipe,"
Battelle-Columbus
Report
to
Bonney Forge, Allentown, PA 18105, Apr. 30, 1981.
14.
Rodabaugh,
E. C. , "Cycl ic B<?nding Tests of a Half-Scale Model of
an
8"
x 24"
Saddle Reinforced Branch
Connection,''
Tube Turns, Report
No. 8.011,
Louisville, K Y 40201, 1953.
15. Mershon, J. L., Letter to member of PVRC
Subcommittee
on Rein
forced
Openings,
Dec. 20, 1963.
16.
Schneider,
R. W.,
Letters to
C. R. Felmley, .Jr., Executive
Secretary of
PVRC,
Mar. 17, 1981, Mar. 31, 1981 and Apr. 10, 1981.
17.
Schneider,
R. W., Letter to
,J.
Millman, Secretary of ASME Section III,
Apr. 21, 1981 (copy to B31 Code Committee on Pressure Piping).
18.
Khan,
A. S.,
"A Study of Fatigue Crack Initiation and Failure
in Rein
forced Shell to
Shell Intersections,"
U. of Oklahoma, Report Prepared for
WFI
International, Houston,
TX,
May
1985.
19.
Lankston, R. J. (Taylor Forge
Engineered
Systems,
Inc., Paoli,
KS
6(l071)
Letter to E.
C.
Rodabaugh
dated May 30, 1985.
20. Mershon, .J. L., et al.,
"Local
Stresses in Cylindrical Shells Due to
External Loadings on
Nozzles-Supplement
to WR Bulletin No. 107,
WRC Bulletin 297,
New York, Aug. 1984.
21. Fujimoto, T. and Soh, T.,
"Flexibility
Factors
and
Stress Indices for
Piping
Components with D T > 100 Subjected to
In-Plane
or
Out-of-Plane
Moment,"
pp.
59-70 of ASME Bound
Volume No.HOO:J29
of Pressure
Vessels
and
Piping Conference, New
Orleans,
.June 1985.
22.
Wordsworth, A.
C.
and Smedley,
G. P.,
"Stress
Concentrations
of
lin
stiffened Tubular Joints,"
European
Offshore Steels Research Seminar, Cam
bridge, 1978.
2:l. Moffat, D. G., "ExpNimental StrP" Analysis of J FabricatPd Equal
Diamc·ter
Branch Pipe Intersections Suhj('('t('(l to Moment Loadings," 'roc.
lnst.
Mech.
Eng . Part A.lsstt<: A4.
24. Wkhman, K. R.
HoppN.
A. and Me"hon . . L., "Local
Spherical
and
Cylindrical Shell> Due to
External
Loadings,"
WRC
/07
NPw York. Aug.
19hfl, ""'ised Marrh 1979.
2f>. Corum,.). M . et a/ "TheorPtiral and Experim<•ntal Analysis of
OHNL Thin-Shell
Cylinder to-Cylinder-Model No. 1
2,
:l, ·ll. OHNL-TM
4:,5:l, fJ021, G020 and f>OJ9 for ModPls I, 2, :
and
4, respectively. Dated Oct.
1972, Oct. 197fJ, ,Jltne 1975
and
,June 197;, for Models I, 2, :land
4,
respectively,
Oak Ridge National
Laboratory,
Oak Hidge. TN
:mno.
26.
Hodahaugh, E. C.
and Moore, S. E.,
"Stress
Indices and Flexibility
Factors
for Nozzles in
Pressure
Vesspls
and
Piping," NUREG/l'H-0778,
Oak
Hidge
National Laboratory,
.June 1979.
27.
Rodabaugh, E.
C.,
"Compari,ons of ASME Code a t i ~ u e
Evaluation
Method
for Nuclear Cla8s
1 Piping with
Class
2
or
3 Piping,"
Nl1HEG/CR
:)24:l. Oak Hidge National Laboratory, .June 1983.
28. Rodabaugh, E. C., "Sources of Uncertainty in the Calculation of Loads
on
Supports on Piping
Systems,"
NUREG/CH-3599, Oak
Hidge National
Laboratory,
.June 1984.
Appendix A-Specific Recommendations for NC-
3600 of
ASME
Code Section III
The
last pages of this Appendix include copies of
pages 166, 171,
172, 173
and
17
4 from NC-3600 of the
ASME Code, Section III, 1986 Edition. Pages
166, 171,
172
and
174 are marked-up
to
show recommended
changes.
Table A1
contains
the
recommended notes to
replace those on
p.
173.
The changes include those in Section 5 of this
re-
port. We will discuss those first in
the
following. In
addition, several more-or-less editorial changes tooth
er portions of Code pages 171, 172 and 173 are suggest
ed; we discuss those subsequent ly in
the
following. To
facilitate the discussion
of
changes, we have numbered
the
"Descriptions" from (1) to (15) as noted on the left
margin of Code pages 171 and 172.
Changes From Recommendations in Section 5 of This
Report
Page
166
This
change reflects Recommendation
IOc).
This
change makes the procedure the same for Descriptions
(4), 5)
and
(7); and eliminates
the t ~ / T r )
term in the
i-equation for checking the branch end of Description
(7).
We have changed
Tb
t o ~ as being consistent with
page 174. We have
not
changed
Tr;
it agrees with page
174
but not
page
171.
Description (4),
Welding
tee
per
ANSI Bl6.9
The only change
is
replacing the meaningless" 1"
by
"Note (9) ; see Recommendation
1).
Description (5), Reinforced
fabricated
tee
The "Description" has been retitled to "Fabricated
branch connection "
rather
than
"tee."
This is mo-
tivated by revised footnote (7), which is applicable to
"Fabricated branch connections "; Descriptions
5)
and
7) not "Welding tee "Description (4). The "1"
has been changed to
"Note
(9)."
I t might be noted
that
the run moment problem
continues to exist for Description (5). For example,
consider a 24 in. diam x 0.375 in. wall run pipe with
4.5
in. diam x 0.237 in. wall branch. For a pad or saddle
with te = 0.375 in., the SIF i =4.57. Using Description
(7), which, of course,
is
without a pad,
i
=
2.1
(lower
bound,
r2
not provided). Perhaps the
Mob
problem also
exists.
36
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Description (6), Unreinforced
fabricated
tee
Deleted, See Recommendation (lOd).
This
De
scription is included in Description (7). Retention of
Description (6) would, of course, continue both the
M
0
t>-problem and the run-moment problem.
Description
(7),
Branch connection
The Description has been retitled to make
it
con
sistent
with
and
distinct from Description (5).
The equations
for
i are from Recommendation
(lOa). Note
that
they are written for
r2
not provided;
i.e., as-welded. For the branch end, when
the
value of i
is not controlled by the minimum,
the
equations for i
reduce the value by a factor of 2 from
the present
rule.
They reduce
the
minimum for
the
branch end from the
present 2.1 to 1.5.
For the run ends, there is no change from the
present rules.
The
factor of 2 in the present footnote
(6)(h) leads to the coefficient 0.8 rather than the
present 0.4. The present minimums of 2.1 for rz not
provided
and
1.5
for
r
2
provided are retained.
However, Description 7) is no longer limited to
r/R
0.5. For
r/R =
1.0, the SIF equation for branch ends
becomes essentially identical to the present i =
0.9 R/
T 213; the difference lies in the r/rp) factor. For r/R =
1.0,
the SIF
equation for run ends becomes 0.8 R/T)213
rather than
the
present 0.9(R/T)213.
There
is a subtle but usually numerically insignifi
cant
change in that Z for run ends and for full outlet
branch connections is not defined as 7r Rm)
2
r or
1r r
2 T ~ . To the extent that a Code user takes
Z
to be
the
exact section modulus, he will have a
bit
higher
calculated stress than if he used the approximate sec
tion modulus.
Present Note
(6)
Part
(a) has been dropped because
it
is
not
neces
sary
and because it implies that branch connections
that
do
ot
meet NC-3643 are somehow acceptable.
Parts (b)
and c)
are picked up in proposed note (7);
applicable to both Descriptions
5)
and (7).
Part (d) has been dropped because moment fatigue
tests
and
theory indicate
that
the inside corner radius
is
not
a critical consideration.
Parts (e) and
h)
have been combined in proposed
note (8).
Part
f)
has been dropped. The lower bound of 1.5
for checking the branch end with
r
2
provided has been
retained.
Part g)
has been dropped because of the D
0
/t
100 limit in the title of Fig. NC-3673.2(b)-1 and be
cause the
r ~ / R
0.5limit no longer applies.
Fig.
NC-3673.2(b)-2, Branch
dimensions
General note
2)
has been deleted; see Recommen
dation
(13). Editorially, an arrow on
rp
in (b) should be
added
and, in (c), the arrow on
rp
should end
at
the
vertical line.
More-or-less Editorial
Changes
to
Fig. NC-367:l.2(b)-l
Note (l)
The
words reinforced thickness were perhaps
meant to be reinforcement thickness but, more di
rectly, te is
the
pad or saddle thickness.
Note
(2)
Proposed footnote
2)
is intended to be the same as
the present footnote
2)
with respect to i-factors. How
ever, the word bending has been changed to mo
ments. See discussion under note 3).
Note
(3)
Proposed footnote
3)
is intended to be the same as
footnote (2) as
it
applies to k-factors for elbows, bends
and miters. However, the word bending has been
changed to
both
in-plane
and
out-of-plane moments
and added: For torsional moments, k
=
1.00. We
think that the word
bending is
meant to exclude
torsional moments; see present footnote (8).
In Description (3),
the
heavy center lines extend
some undefined amount;
an
ambiguity
we
do
not
at
tempt to correct.
Note
(4)
Proposed
note
4) is
the present
note (3), with the
second line deleted. Fig. NC-3673.2(b)-5 (and
-4)
are
deleted in accordance with recent action of the ASME
Code, Working Group on Piping.
Note
(9)
We propose that this note be deleted. Problems with
over-thickness elbows have arisen with wrought steel
elbows;
ot cast
elbows.
Note Tie-ins
The present note tie-ins are incomplete. Note 9) is
not
shown with Description (1). Note
2)
should be
tied into Descriptions (5), (6), (7),
12) and
(13) as well
as
(1),
(2),
3)
and 4); i.e.,
i
1.0
applies
to
all of these
descriptions.
In
the proposed revisions, we have at
tempted to provide complete note tie-ins.
Flexibility Factors
Proposed note
3)
applies
to
elbows, bends
and
mi
ters. Proposed note
9)
applies to Fabricated Branch
Connections and Tees.
The
1 for Descriptions
8)
through (14) is meaningless and should be deleted.
Perhaps a
note
can be developed which indicates the
intent of
the
Code for these descriptions
but we
have
not
attempted to
do so.
Description
(12), 30
deg.
tapered transition
The relevant portion of ANSI Bl6.25 is now Fig.
NC-4250-1.
Description
(15), Corrugated straight
pipe or creased
bend
This Description, Corrugated straight pipe or cor
rugated or creased bend, and the equivalent of
present note (8), are unchanged from the 1955 edition
Stress Intensification Factors
37
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of B31.1. At
that
time (and still in B31.1):
Calculations shall take into account stress intensi
fication factors found to exist in components other
than plain straight pipe. Credit may be taken for the
extra flexibility of such components. In the absence
of more applicable data, the flexibility factors and
stress intensification factors shown in Fig. 2 may be
used.
Fig. 2 contained much
of
what is now in Fig. NC
3673.2(b)-1 including Description (15).
Figure NC-3673.2(b)-l, in
our
view, is different from
B31.1-1955 in
that
it
is part
of an enforced
set
of rules.
The
piping system analyses and stress calculations are
subjected
to
checking; which means
that
two or more
readers
of the
rules
must
be able to agree on
the
signifi-
cance of the rules. For Description (15),
it
appears
impossible for ny reader to say
what
the significance
is.
To
illustrate the point, suppose we
put
a single cor
rugation, with depth equal to
the
wall thickness, in a
40 foot length of pipe. Is the flexibility factor of
this 40
foot length of pipe equal to 5?
f
not, using =5 might
make
the piping system analysis (including support
and
nozzle loads) almost meaningless. On
the
other
extreme, in what quant itat ive way is a corrugated pipe
different
from a Bellows Expansion Joint, NC
3649.2?
We have deleted Description (15).
f
a need exists
for this Description,
we
deem it essential
that it
be
quantified so
that
a reader will know what the k 5
and i = 2.5 are applicable to.
Table Al: Revised Notes for Fig. NC-3673.2(b)-1
on
Page
173
(1) Same as
present
note 1) , except
te
=
pad
or saddle
thickness, in .
(2)
Stress
in tens i f ica t ion
factors,
i , apply to moments in any plane and
shal l
in
no
case be taken
as less
than 1.00 except that for branch leg
checks
of welding tees
and
fabricated
branch
connections reinforced
by
pad
or saddle,
i T ~ / T r ) )
1.0.
3 )
Flexib i l i ty
factors ,
k,
apply
to both
in-plane
and
out-of-plane
moments
and
shall
in no case be taken
as l ess
than
1.00.
For torsional moments,
k
=
1.0. The factors apply over the effect ive
arc length
(shown by
heavy center
l ines
in the sketches) for elbows, bends and miters.
(4)
\ ~ h e r e flanges
are attached
to
one
or
both ends,
the
values
of k and i
shal l
be multiplied by the factor c given
below:
(a) One end
flanged,
c = hl /6
(b)
Both ends
flanged, c
= hl /3
But after such multiplicat ion, values of k
and
i shal l not
be
taken as
less than 1.00.
(5) Same
as
present note (4).
(6) Same
as
present note (5).
(7) Fabricated branch
connections:
38
(a) Stress
in tens i f ica t ion
factors
are applicable only where the axis
of the
branch
pipe is normal to within ~ 5 ° of
the
surface of
s t ra ight
run
pipe.
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Table Al.Continued
b) Stress
in tens i f ica t ion
factors are based on t es t s and/or
theories
in
which the branch connection is
in
s t ra ight run pipe with about
two or more diameters of run
pipe
on each side of the
branch.
The
effect
of
closely spaced branch connections may require special
consideration.
8) Fabricated
branch
connections
other
than
pad
or saddle reinforced:
If
a radius
rz is provided that i s not l ess than
the
larger
of
Tb/2, Tb y)/2 [Fig. NC-3673.2 b)-2 sketch c)] or
Tr/2,
then
calculated values of ib and
i r may
be divided by 2.0; but with
i b T ~ / T r )
1.5
and
i r
1.5.
9) Fabricated
Branch
Connections and Tees:
the
In
piping
system analysis, i t may
be
assumed
that
the f lexibi l i ty
is represented by a
r igid
joint
at
the branch-to-run centerlines
juncture. However, the Code user
should be aware that this
assump
t ion
can be
inaccurate
and
should
consider
the
use of
more
appro
priate
f lex ib i l i ty
representat ion.
10)
Same
as
present note
7).
11) Same as present note 10).
12)
Same
as
present note 11).
13)
For checking branch leg:
F o r
;: <
0 , 9 :
1.5 - - -
_
Rm)2/3 ~ ) l / 2 ~ )
Tr
m rp
i T ~ / T r ) 1.5
F o r ~ : ) = 1.0:
i =
0.9 ( ~ t
c;
Linear
interpolation is to be used for : : )be tween 0,9 and 1,0
For
checking run legs:
i
=
0.8
~ ~
2 1 3
;:);
2,1
minimum
Stress
ntensification Factors
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NC-3653.3-NC-365H.l
SECrJON
III. DIVISIO: ' 1 -
SUBSECTION
NC
1986
Edition
M
•.
M •. .H, . •H,, =
r run
pipe mean cross-sect ional radius, in. ·
r ,., =branch mean cross-sectional radius, in.
U se
i T b / T r )
i n p l a c e
o f
i;
b u t
n o t
less t h a n
1.0.
z
n(C )2
'
i
3
m b , n .
,=effective
branch wall thickness,
=lesser of T or iT
Tb
nomina
ranch wall thickness, in.
,=nominal wall thickness of
run
pipe, in.
For
the ~ , use M •
Ms.
and
omit
l egs
Me
as
defined in NC-3633.3(a);
I
fllfa
Z
for
the run pipe
NC-3654
Consideration of
Level C Service
Limits
For Service Loadings for which Level C Service
Limits are
designated,
the conditions of
Eq. (9) shall
be met.
In calculating the
resultant
moment
loading
M
8
), the
effects
of anchor
displacement
due to
earthquake
or
other
secondary effects need not be
included.
The allowable stress
to
be use for this
condition is
2.25S
but
not greater than 1.8Sr
S = basic material yield strength at Design T em
perature, psi
Sit= basic material allowable stress at Design
Temperature,
psi
NC-3655
Consideration
of
Lenl
D Service
Limits
For
Service Loadings for
which
Level D Service
Limits are
designated,
the conditions of
Eq.
(9) shall
be met. In
calculating the
resultant
moment
loading
M ) ,
the effects of
anchor
displacement
due
to
earthquake or
other
secondary effects need not be
included. The allowable stress to be use for
this
condition is
3.0S
but
not
greater
than 2.0S,
S_,=basic
material yield
strength
at Design
Tem-
perature.
psi
Sit=
basic
material allowable stress at Design
Temperature, psi
NC-3658
Analysis of Flansed Joints
Flanged
joints
shall be
analyzed
for compliance
with one of the
fo11owing
subparagraphs.
NC-3658.1 Any Flanged Joint. Flanged joints may
be analyzed
and the
stresses evaluated by using
the
methods given in Appendix XI as
modified by (a)
166
4
WRC Bulletin
329
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1986
Edition
o..t.<:
phon
W e l d i n < ; ~ elbow or
pi pe
bend [Notes (3)1
1), 2), 3), 4)]
ClOMiy apa<:..:l mi1er
bend [Notes
(1) ,
( 2) . ( 3) . (
4)
J
s
< r l
+ t a n 0)
hend [Notes 1), 2),
( 3). ( 4 . ( 5 l
s r ( l +tan 9)
Weldtng
11111
per
ANSI
8113.9 [Notn (1), 21)
F a b r i c a t e d branch
c onne c t i on r e in fo rced
wi t h pad o r
sa d d le
[N o t e s (1 ) , ( 2 ) , ( 6 )
7), 11)]
Unreinforce<l
fabricat..:l
IM
( N o t (1), (10))
Fle.•b•hty
C h a r a c ~ H I I t • c
t.R
r>
1t.
cot
2r
t. (1 +
cot
IJ)
2r
4 4
r.
---
r.
+ .,,
r l .
)''•
NC-3<XXl
-
DESIGN
Flex•b•l•ty
Factor;;
1.65
h
1.52
1.52
,
Note ( 9 )
Note (9)
Streu lnt< na•·
f•caflon Factor t
0.9
0.9
0.9
0.9
0.9
h t.
tlg. NC-3673.2(b)-l
Ske Ch
FIG. NC-3673.2(b)-l FLEXIBILITY
ND
STRESS INTENSIFICATION FACTORS (0
0
It . s 100)
171
Stress Intensification actors
Omit
41
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@
@
42
O...c.rtphon
Fa b r i c a t e d
branch
con
n e c t io n
ot he r
than Fad
or sadd le r e i n fo rc e d
[Notes
7 ) , (8))
Girth
bun
w•ld
[Not•
(II]
r. l 0.237 ln.
Gonh
butt
wald
[Not•
(II)
t
< 0.237
In
t
' 'r ' efentlal ftUM w.Sded
w.ld..:l
101nta
N•·'
e (
12) )
ra . ..
to•nt
SECfiON 111. DIVISION I
SUBSECTION NC
F&e••btftty
Fa<1or t
Note
9 )
I
StrHI
lnt•natfic•hon
Fa<1or 1
Note
( 1 3 )
I 0
1.9
mal<.
r
o 9(1 + 36/r.l
but
not la11 than 1.0
2.ti(C,It .l
but
t\01
••• than 1.3
2.1
1986
E ~ i t l o n
Skelch
Fill NC·Je73.21bl·2
Ftg
NC-4427
1
lll<atchH lc·1),
(c-2).
and
(<:·3)
fig. NC-4611·1
r · ~ ~ r 1
I
3Ci
deg
taper..: tran•lfk>n
[Notes
(1),(2)]
~ a f l t r i e
enrl .eeantrie
r ed u ce r s [Notes
(1)
(2)
( 1 0 ) )
(ANSI B16.9)
Threadotd p i ~ joint
or threadotd l ~
t .l .. 0.0036
£, + u .
r
'·
2.0
mu. Of
0 ) '"
.5 + 0.01o ::::
•
2.3
Fia .
NC-4250-1
.f __
I f ~ *
.
o
Omit
FIG. NC-3673.2<b>-l FLEXIBILITY AND STRESS
INTENSIFICATION
FACTORS
(0
0
It . s lOO)(CONT O)
172
WRC Bullet in 3 9
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1986 Edition
NC-3000 - - DESIGN
Fig:. NC-3{)73.2(b)-1
FIG. NC-3673.2(bl-l <CONT Dl *
NOTES:
( 1) The following nomenclature applies
r
=
mean radius
of p1pe.
in. {matching
pipe
for tees
and elbows)
t =
nommal wall thickness
of pipe. in. [matching
pipe for
tees
and
elbows. see
Note (9)]
R
= bend
radius
of elbow or pipe bend.
in.
8
=
one-half
angle
between adJacent
miter axes.
deg.
s = miter
spacing
at center l ine. in
r. =
reinforced
thickness.
in.
13
=average perm1ssible
mismatch at girth
butt
welds
as
shown in
Fig.
NC-4233-1. A value of 131ess than
Y in.
may
be used provided the smaller mismatch is specif ied for fabricat ion. For
f lush
welds.
as defined
in
Fig.
NB-
368
3. 1
cl-1, b
may
be
taken
as zero.
i =
1.0,
and flush
welds need not be ground.
D.
outside diameter.
in.
(2)
The
flex1bility factors
k and stress
intensif ication
factors apply to
bendmg 10
any plane for
fittings
and shall in no
case be
taken
less than unity.
Both
factors apply
over the
effect ive arc length
(shown
by heavy center l ines in the
sketches)
for curved
and miter elbows.
and
to
the
intersectiOn pomt
for
tees. The values of
k
and i
can
be read directly
by entering
with
the characteristic h
computed
from the equations given.
(3) Where f langes
are
attached to one or
both
ends. the values of k and i shall be corrected
by
the factor c given below.
which can be read d1rectly from
Fig.
NC-3673.2(bl-5. entering with
the
computed
h.
(a)
One end
f langed.
c
=
h '•
(b)
Both ends
f langed.
c =
h
'>
(4)
Also includes single
m1ter jomts
(5)
When
t 1
5r
_
h =
4
05 r J r
(6) The equat1on applies
only
if
the
fo l lowmg
cond1tions
are met
(a)
The
re1nforcement area requ1rements of NC-364 3
are met
(b)
The
ax1s of the branch pipe 1s normal to the
surface
of run p1pe waiL
(c)
For
branch
connections in
a p1pe. the
arc distance
measured
between
the
centers
of
adJaCent branches
along the
surface of the
run p1pe is
not less
than
three
t imes the
sum of
t h e ~ r mside radii in the
longitudinal direction
or
not
less
than
two
t imes the sum of the1r inside radii along the
circumference
of the run pipe.
(d) The ms1de corner radius r [F1g N C - 3 6 7 3 . 2 b ~ 2 ]
for
nominal branch pipe
size
greater than 4 m. shall be between
10%
and 50% T The
radius
r is not
required for
nominal branch pipe size smaller than
4
in.
(e)
The
outer rad1us r IS
not less than the larger of T.l2. (T - Y)/2 (Fig.
NC-3673-2(bl-2 sketch
(c)] or
T,/2.
(f)
The outer radtus r IS not less than the larger of
1)0002/ ldo
(2) 2
s1n
II)'
t1mes
the
offset for the
conf1gurat1ons
shown in F1g NC-3673
2(bl-2
sketches
(a)
and
(b).
(g)
R_ T,
·
50
and
r
_ R ~ ·; 0.5
(h)
The
outer rad1us r, IS not reqUired
prov1ded
an add1t1onal mult1pller of 2.0 IS mcluded in the equations for branch
end and run end stress intens1ficat1on
factors
In this case.
the
calculated value
of
i
for the
branch
or run shall not
be less than
2 1
(7)
The equat10n applies only
if
the follow1ng condit ions are met
(a)
Cone
angle n
does
not exceed
60 deg.
(b)
The
larger
of D, I
r,
and
D
I r,
does
not exceed 100
(c)
The
wall
th1ckness
is not
less
than r,
throughout the body of
the reducer.
except in and immed1ately
adJacent to
the
cylmdr1cal
port ion on the
small
end. where the
th1ckness
shall not be
less
than
t,.
(d) For eccentnc reducers. a is the maximum cone angle
(8) Factors
shown
apply to
bending;
flexibility
factor for torsion equals 0.9.
(9) The designer is
caut1oned
that cast
butt welding elbows may
have
considerably heav1er
walls
than that of
the
pipe
with wh1ch
they
are used.
Large errors may
be
introduced
unless
the
effect
of these greater thiCknesses is considered
( 1
0) The stress mtens1flcat10n factor i shall in no case be
taken as
less than
2 1
( 1 1)
C. the
f1llet weld
length. For
unequal
leg
lengths.
use the
smaller
leg length for C.
See
abe l Al for proposed changes .
Stress Intensification Factors
43
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f la. NC-3673.2(b)-2
SECTION Ill. DIVISION l - SUBSECTION NC
enr l h r
- Branch
do
,.
m
T
b
P
Tb
(c)
(at
Ll
''J
,
Rm
;p
2
r b · r b • 0 6 6 7 v
o
45°
d • outttdtt
dtameter of
branch P•Pe.
tn
r ...
..
mean r1d1u1
of branch P•P<& m
do
,,
m
Br&nch
T
b
]
p
r,
Branch
GENERAL
NOTH
f f ~ < ~ t
1
Rm
(bl 2
(dl
1986 Edition
dd
r r ow
r·
'
nom.nal thtckneaa of brench p pea,
'
R_ • mean radtul
of run
ptpe.
'
( 2} If L ~ l t U t l s Of f )((f l'f" 'd" 0 s \ r
r
then r .. can be t.aken
th t '
' dnJ S 10 thf"'
t ...
ntttt
of T
T • nomtnal th•cknet-a
of
run P'f:M l'.
tn
FIG. NC-3673.2(bJ-2 BRANCH DIMENSIONS
174
WRC
Bulletin
3 9
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250 Generalized Yield Surfaces for Plates and Shells, by D B. Peterson, W. C. Kroenke, W. F. Stokey, and W. J. O Donnell, July 1979.
251
Comparison
of Three-Dimensional
Finite
Element and
Photoelastlc
Results
lor
Lateral Connection,
WC-12B2,
August 1979.
252
Ultrasonic
Evaluation and Sectioning
of
PVRC
Plate
Weld
Specimen
201, by A. C. Adamonis and E.
T
Hughes, September 1979.
253 A
Survey
of Simplified
Inelastic
Analysis
Methods,
by K E Nickell, October 1979.
254
( 1) A
Critical Evaluation
of
Plastic Behavior
Data and a
Unified Deflnltlon of
Plastic Loads for Pressure
Components,
by
J.
C Gerden;
(2)
Interpretive Report
on Limit Analysis
and Plastic Behavior
of Piping Products by E. C. Rodabaugh; (3) Interpretive Report on
Limit
Analysis of
Flat Circular
Plates, by W. J.
O'
Donnell,
November
1979.
255
Experimental
Investigation of
Commercially
Fabricated 2:1
Ellipsoidal
Heads Subjected to Internal Pressure, December 1979.
256
Review of
Data Relevant
to the
Design
of
Tubular
Joints
tor
use
In
Fixed
Offshore Platforms, by
E
C. Rodabaugh, January 1980.
257
Analysis of the
Ultrasonic
Examinations of PVRC Weld
Specimens
155,
202 and
203 by Standard and
Two-Point
Coincidence Methods, by
R
A. Buchanan
and 0. F. Hedden, February 1980.
258 International Benchmark Project on Simplified Methods for Elevated Temperature Design and Analysis: Problem 1-The
Oak
Ridge Pipe Ratchetlng
Experiment; Problem
l i The Saclay Fluctuating
Sodium
level
Experiment,
by H. Kraus, May 1980.
259 Analysis
of
the Radiographic Evaluation of PVRC Weld Specimens 155, 202, 203, and 251J, by
E
H. Ruesche r and
H
C. Graber, June 1980.
260
Energy Dissipation
Characteristicsof
Pipes
and
Short
Compression Members
as
Elements of Pipe-Whip
Restraint,
by
S.
S. Palusamy, R
L
Cloud, and
T.
E.
Campbell, August 1980.
261
Effects
of Porosity on
the Fracture
Toughness
of
5083,5456, and 6061 Aluminum Alloy Weldments, by W. A. McCarthy,
Jr.
H. Lamba and F. V. Lawrence,
Jr.
September 1980.
262 ( 1}
Derivation of
ASME Code
Formulas for the
Design
of Reverse
Flanges, by E. 0. Waters and
R.
W. Schneider. (2) Functional Test of a Vessel with Com-
pact Flanges In
Metal-to-Metal Contact,
by J.
Webjornand
R. W. Schneider,
(3) Interpretive
Report on
Gasket
leakage Testing, by H. Kraus, October 1980.
263 An Annotated
Bibliography
on
the
Significance, Origin and
Nature
of Discontinuities In Welds, 1975-1980, by C. D Lundin and S.
J.
Pawel, November 1980.
264 The Influence
of Mulllaxlal Stress on
low-Cycle
Fatigue
of
Cr-Mo-V
Steel
at
1000 °F,
by
fl.
H.
Marloff
and R. L Johnson, December 1980.
265
Interpretive
Report on Small-Scale
Test
Correlations
with
Oata,
by
R
Roberts and
C.
Newlon, February 1981.
266 Weldability and Fracture Toughness of 5 Nl Steel-'Part
1:
Weld Slmulatloo Testing, by A. Ohooge,
K
Ostyn, W. Provost and A. Vinckler, Welda-
bility
and
Fracture Toughness of 5
Nl
Steei-'Part 2:
Wide
Plate Testing, by A. Dhooge, W. Provostarrd A. Vinckier, Aprll1981.
267 Elastic-Plastic
Buckling
of internally Pressurized
Ellipsoidal
Pressure
Vessel Heads, by D. Bushnell,
May
1981.
268
Review of Worldwide Weld Discontinuity Acceptance
Standards, by C. D. Lundin, June 1981.
269 Interpretive Report on Dynamic Analysts of Pressure
Components-Second
Edlllon, August 1981.
270
Long-Range Plan
for Pressure-Vessel
Research-Sixth
Edition
by
the
Pressure Vessel Researdl
Committee,
September 1981.
271 ( 1} Methods
of Analysis of Bolted Flanged
Con-ct ions-A Review,
by
A. E
Blach
and A. Bazergui (2)
Gasket leakage
Behavior Trends, by H D. Raut, A.
Bazergui andL Marchand, October 1981.
272 ( 1
Design
of Beam
Columns
with ateral-Torsional End Restraints, by
T. L
Hsu and G.
C.lee
(2) Tapered
Columns
withUnequal Flanges, by G.
c.
Lee and T.
L
Hsu,tlovember 1981.
273 Design
Implications
of Recent Advances In ElevatedTemperature Bounding Techniques, by J. S. Porowski, W.
J.
O Donnell and M. Badlani, December 1981.
274
International
Benchmark Project on Simplified
Methods
for Elevated Temperature Design and Analysts: Problem The
Sactay
Fluctuating Sodium
level
Experiment;
Comparison of Analytlcill
and Experimental
Results; Problem
lii_.:.The
Oak Ridge
Nozzleto
Sphere
Attachment,
by
H. Kraus, January 1982.
275
The Use
of
Quenched and Tempered
214
Cr-1
Mo
Steel
for Thick
Wall
ReactorVesselsln
Petroleum
Refinery
Processes: An
Interpretive
Review
of
25
Years
of Researdl and
Application,
by W. E.
Erwin
and J.
G.
Kerr, February 1982.
276
A Summary
and Critical Evaluation of
Stress ntensity Factor
SolutlonsDfComer Cracks
at
the Edge Dl
a
Hole, by
R L Cloud and S. S. Palusamy,
April
1982.
277 High Temperature Properties of
214
Cr-1
Mo
Weld
Metal, by
C. D
Lundin,
B. J.
Kruse and M.
R.
Pendley,
May
19S2.
278 The Crack Arrest
Properties
of 9 Nickel Steels for
Cryogenic
Applications, byRD. Stout and A. W. Pense, June 1982.
279
Weldablllty and Fracture TDughness of
Quenched
and
Tempered
9 Nickel
Steel: Part
1-Weld
Simulation
Testing;
Part 11-Wlde
Plate Testing by
A.
Dhooge, W. Provost
and A. Vinckier, July
1982.
280 The Varestralnt Test, by C. D Lundin,
A.
C.
Lingenfelter, G.
E.
Gmtke,
G
G. Lessmarln and S. J. Matthews, August 1982.
:281 Hydrodynamic Response
of
f luid
Coupled Cylinders:
Simplified
Damping and Inertia
Systems, by S. J. Brown, October 1982.
282 Elastic-Plastic Buckling
of
Axially
Compressed
Ring
Stiffened
Cyllnders•Test vs. Theory, by D Bushnell,
November
1982.
283
A Critical Evaluation Df Fatigue Crack Growth Measurement Techniques for Elevated Temperature Applications, by
A E.
.Carden, February 1983.
284
The
External
Pressure Collapse Tests of Tubes, by
E
Tschoepe and J.
R.
Maison, 1983.
285
( 1 Stress ndices and Flexibility Factors
for
Concentric
Reducers, by
E
C.
Rodabaugh and
S.
E
Moore
(2) Finite
Element
Analysis of
Eccentric Reducers
and Comparisons with Concentric Reducers
by
R R Avent, M.
H:
Saddand E.
C
Rodabaugh, July 1983.
286
fatigue
e h a ~ i o r of
Aluminum
Alloy
Weldments,
by W. W. Sanders, Jr. and
R H.
Day, August 1983.
287
Welding
of
Copper and
Copper Base Alloys,
by R
J.
C.
Dawson, September 1963.
288
Fracture
DfPlpellnes and
Cylbuiers Containing
a
Circumferential
Crack, by F. :Erdogan and H. Ezzat
October
1983.
289
Hot
Cracking.Susceptlblllty
of Austenitic
Stainless
Steel Weld Metals, by C. D Lundin and
C.
P
D Chou, November 1983.
290 Factors
Affecting Porosity
In Aluminum Welds-A Revlew;by J. H. Devletlan and W. :E Wood, December 1983.
291
Fracture
Control
of Pressure Vessels U p
to 216
Inches Thick,
by P.
0.
Metz, January 1984.
292 PVRC Milestone Gasket Tests-First Results, by A. Bazergui and
L
Marchand, February 1984.
293 Current Welding
Research
Problems, Compiled and Edited by R. A. Kelsey, G. W. Oyler and C. R. Felmley, Jr., April 1984.
294 ( 1) Creep of Bolted
Flanged
Connections, by H Kraus and W. Rosenkrans (2) Short
Term
Creep and
Relaxation
Elehavlor
of
Gaskets, by A. Bazergui, May
1984.
Listing continued on outside back cover
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295 Fundamentals of Weld Discontinuiti es and Their Significance, by C. D. Lundin, June 1984.
296 Fitness-for-Service
Criteria for
Pipeline Girth-Weld Quality, by R P. Reed,
M. B
Kasen,
H.
I, McHenry, C. M. Fortunko. and
D.
T.
Read,
July 1984.
297 local Stresses In Cylindrical Shells Due to External loadings on Nozzles-Supplement to WRC Bulletin No. 107, by J. L Mershon, K Mokhtarian, G. V. Ran-
jan, and E. C. Rodabaugh, August 1984.
298 long-Range Plan
lor
Pressure-Vessel
Research-Seventh
Edition, by the Pressure Vessel Research Committee, September 1984.
299
1) Engineering Aspects of CTOD
Fracture
Toughness Testing, by G.
W.
Wellman and
S.
T. Rolfe; 2) Three Dimensional Elastlc·Plastlc Fi nite Element
Analysis of Three-Point Bend Specimen, G. W. Wellman. S. T. Rolfe and R. H. Dodds; and
3)
Failure Prediction of Notched Pressure Vessels Using the
CTOD Approach, by
G.
W. Wellman, S.
T.
Rolfe and R. H. Dodds, November 1984.
300
(
1)
Technical Position
on
Criteria
Establishment;
2)
Technical Position on Damping Values for Piping-Interim Summa ry Report;
3)
Technical Position on
Response Spectra Broadening;
4)
Technical Position on Industry Practl<:4, December 1984.
301 A
Parametric
Three-Dimensional
Finite Element
Study of
45
Degree
Lateral
Connections, by P. P. Raju, January 1985.
302
1)
Postweld HeatTreatment
of Pressure Vessels, by
R. D
Stout; 2) Relaxation Stresses In Pressure Vessels, by P. S. Chen, W. A. Herman, and A. W. Pense;
3) A Study of Residual Stress In Pressure Vessel Steels, by R J. Zhou, A. W. Pense, M. L Basehore. and D
H.
Lyons, February 1985.
303
Interpretive
Report on
Dynamic
Analysis of Pressure Components-Third Edition-April 1985.
304 Experimental Limit Couples for Branch Moment loads on 4-ln. ANSI B16.9
Tees
by J Schroeder, May 1985.
305
Summary Reports Prepared by the JPVRC Subcommit tee
on
Hydrogen Embrlttlement: 1) Hydrogen Attack Limit of 2'/. Cr-1 Mo Steel by Task Group I; 2)
Embrittlement of Pressure Vessel Steels in High Temperature, High Pressure Hydrogen Environment by Task Group II;
3)
Hydrogen Embrlttleme nt of
Bond
Structure
Between Stainless Steel Overlay and
Base
Metal by Task Group Ill, June 1985
306
PVRC Flanged Joint User Experience Survey by J.
R
Payne, July 1985
307 Fatigue and Creep Rupture
Damage
of Perforated Plates Subjected
toCyllc
Plastic Straining In Creep Regime, by M.L Badlanl, T. Tanaka, J S. Porowskl and
W. J. O'Donnell, August 1985
308 Verification and Application of an Inelastic Analysis Method for lMFBR Piping Systems, by H. D. Hibbitt and E. K Teung, September 1985
309
Development
of
a Production Test Procedure
for
Gaskets,
by
A. Bazergui,
L
Marchand, and
H.
D. Raut, November 1985
310 Damage Studie s in Pressure Vessel Components, by
F
A. Leckie, December 1985
311 Assessment of the Slgnlflcance of
Weld
Dlscontlnutles: Effects of Microstruc ture and Discontinuities upon Fracture Morphology, by
C.
0. Lundin and C.
R.
Patriarca, January 1986.
312
Joining of Molybdenum Base
Metals
and Factors Which Influence Ductility,
by
A. J. Bryhan, February 1986
313
Computer
Programs
for
Sensitivity Analysis of Stiffened Cylindrical Shells, y R L Clterley, April 1986.
314
Bolted
Flanged Connections
with Full
Face Gaskets, by A. E. Blach,
A.
Bazergul, and R. Baldur, May 1986.
315 Stress Rupture Behavior of Postweld Heat Treated 2-'\'
4
Cr-1Mo Steel Weld Metal, by C. D. Lundin, S.C. Kelley, R. Menon, and B. J Kruse, June 1986
316
1)
Technical
Position
on
Piping
System
nstallation Tolerances,
byE.
B. Branch, N. Kalyanam, D. E Landers, E
0.
Swain, andD A. VanDuyne;
2)
Technical
Posttlon
on
Damping Values tor Insulated Pipe-Summary Report, by J 1 Bitner, S. N. Hou, W. J. Kagay, and J. A. O'Brien, July 1986.
317 PVRC Ce ntrifugal Pump..Piplng Interaction Experlen<:4Survey, by J.
R
Payne, August 1986.
318 ( 1) Factors Influencing
the
.Measurement
of
Ferrite Content In .AustenltlcStalnless.Steel Weld Metal using Magneti c Instruments, by E. W. Pickering,
E
S
Robitz, and D. M. Vancter:griff;(2) Measurement
of
FerriteContentln.Austenlllc Stainless Steel Weld
Metal
Giving Internationally Reproducible Results, by
E
Stalmasek, September 19 86.
319 .Sensltlzation·1lf Austenitic Stainless
Steels;
Effect1>f Welding Variables on
HAZ
Senslllzatlon of AlSI304
and
HAZ Behaviorof BWR Alternative
Alloys 316
NG and 347,
by
C. D. Luctin,
C.
H.
Lee,
A.
Menon, and
E
E. Stansbury, November 1986.
320 Welding Metallurgy and
Weldabllity
of High Stren.Qth Aluminum A lloys , by S. Kou December 1986.
321 The Dynamic Deformation of Plplng, by J L. Mclean,P K. Beazley and A. H. Manhardt, January 1987.
322
1) The Strain
Aging Behavior of
Microalloyed
Steels,by W.
A.
Herman, M.A.Erazo, L R Depatto, M. Sekizawaand A.W. Pense; 2) The
Fracture
Toughness
Behavior
of
ASTM A737 Grade
Band
Grade CMicroalloyed PresSure Vesse l Steels, by J. A. Aadland, J.
l.
Qureshi and A. W. Pense;
3)
The Fracture Be
havior of ASTM
A737
Grade Band Grade CMicroalloyed Steel Weldments, by J M. Aurrecoechea,
B.
Oain and A. W.Pense; {4) Long
Time
Stress Relief
Effects In ASTM A737 Grade Band Grade CMicroalloyedSteels, b yN. Shinohe, M.
SeklzawaandA.
W. Pense,
April1987.
323
Monograph on
Narrow-Gap
Welding
Technology, by V, Malin, May 1987.
324
Investigation
of
Design
Crlleria for Dynamic Loads
on
Nuclear Power
Piping,
by
R. J. Scavuzzo and P.
C.
Lam, June 1987
325 Further Gasket
Leakage
Behavior
Trends, by A. Bazergui, L Marchand andH
0.
Raut, July 1987.
326
Revised Bulletin 191-August 1987. Suggested Arc-Welding Procedures for Steels Meeting Standard Specifications, by C.
W.
Ott and D. J. Snyder. This
Revision is a part onne WAC book, Weldability
of
Steels-Fourth Edition.
Revised
Bulletin 297. Local Stre.ss'es
ln
Cylindrical ShellsDue
to
ExternalLoadings on Nozzles-Supplement
to
WRC Bullet in 107 (Revision
1 , by
J L. Mershon, K
Mol<htarian, G. V. Ranjonand E. C. Rodabaugh, September 1987.
327
Long,Range Plan for Pressure-Vessel Research-Eighth Edition, by the Pressure Vessel Research Committee , October 1987.
328
1)
SpeCimen ThicknessEffects for l a s t i c P i a s t i ~ C T O D Toughness ofanA36 Steel, by G. W. Wellman,
W.
A. Sorem,
R
H. Dodds, Jr., and S. T. Rol fe; 2) An
Analytical and Experimental Comparison
of
Rectangular and Square CTOD Fracture Specime ns of an A36 Steel,
byW.
A. Sorem, R H. Dodds, Jr., and S.
T. Rolfe, November 1987.
329
Accuracy of Stress Intensification
Factors
for Branch Connections, by E. C. Rodabaugh,
December
1987.
Copyright© 1987 Welding Research Council
Requests for reproduction or republi cation permission should be addressed to the
President and Executive Director, Welding Research Council.