ML20115A960
| ML20115A960 | |
| Person / Time | |
|---|---|
| Site: | Wolf Creek  |
| Issue date: | 04/05/1996 |
| From: | WOLF CREEK NUCLEAR OPERATING CORP. |
| To: | |
| Shared Package | |
| ML20115A947 | List: |
| References | |
| GL-95-07, GL-95-7, XX-M-040-R01, XX-M-40-R1, NUDOCS 9607090150 | |
| Download: ML20115A960 (36) | |
Text
. _ . . - .
e Enclostra to WO 96-0107 l ENCLOSURE Calculation of the analyses, thrust and actuator capabilities of EMHV 8802A/B I
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9607090150 960703 PDR ADOCK 05000482 P ppg
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l* FORM APF 05D-00101, REV. 00 CALC NO. MM CALCULATION COVER SHEET ggym, WA 1 #
$ SHEET 1 OF 33
- CALCULATION STATUS PRELIMINARY COMMITTED SUPERSEDED VOIDED
@ FINAL 4
DESIGNATION:
! CLASSIFICATION: X SAFETY-RELATED SPECIAL-SCOPE NONSAFETY-RELATED
! COMPUTER CODENERSION:
N/A CALCULATION
SUBJECT:
Pressure Locking Evaluation for Susceptible Valves Per GL 9547 i
j DESCRIPTIONIREVISION
SUMMARY
- 'I a .
This calculation determines the maximum bonnet pressure that can be accommodated by valves i EJHV8811 A/B, EJHV8840, EMHV8802NB, and ENHV0001/7 with their current motor capability and with l consideration for the limeng co rg,ent.
l Revision 1 of this calculation provided additional margin to the pullout forces to account for diagnostic 1
inaccuracies and the repeatability of this load. In addition, valve EJHV8840 was assumed to have 2,300 psiin the bonnet due to check valve testing performed during Refuel Vill per reference V (see also reference Y). With this pressure assumed in the bonnet and the weaklink increased, the total force required was calculated to d ;
, determine what the load would be for manual operation of the actuator. 418 i
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REV. ORIG /DATE VERF/DATE
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l FORM APF 0$D40102. REV. 00 I
CALC NO. XXM CALCULATION SHEET .,on ,o, o I
SHEET 2 OF 33
- TABLE OF CONTENTS
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En98
- 1. PURPOSE / INTENT 2
- 11. METHODOLOGY 2 i lli. DESIGN INPUTS / ASSUMPTIONS 2 IV. CALCULATION 2 V. RESULTS / CONCLUSIONS 10
- VI. REFERENCES 10 Vll. ATTACHMENTS Attachment A Pressure Locking Testing at Commonwealth Edison 11 1 Attachment B Westinghouse intamal Valve Dimensions 28 Attachment C Anchor / Darling intomal Valve Dimensions 31 5
Attachment D independent Verification 33 Attachment E Westinghouse Maximum Valve Allowable Thrust for EJHV8840 l SW j l. PURPOSE / INTENT H a
- The purpose of this calculation is to determine the maximum bonnet pressure due to pressure locking that valves EJHV8811 A/B, EJHV8840, EMHV8802A/B, and ENHV0001/7 can overcome based on their current capability and
' q.(.O limiting component. This determination supports the evaluations necessary in accordance with Generic Letter (95-
- 07) on pressure locking and thermal binding. Reference Letter WO 96-0023, PIR 95-0313, PIR 95-2170, and PIR 96-1099. %
- 11. METHODOLOGY l 4
The methodology being used was developed by Commonwealth Edison (Comed) and is outlined in Attachment A.
Ill. DESIGN INPUTS / ASSUMPTIONS The design inputs are referenced next to the appropriate line in the body of the calculation in Section IV. The references can be found in Section VI.
The basic concept of this phenomenon is that pressure builds in the bonnet and is sealeo in by the disc. The lesser of the open torque output capability of the motor / actuator and the limiting cc,1,ycr,6 cit (either the valve or actuator) determines the maximum amount of pressure that can be overcome in the bonnet. The current thrust / torque calculation for each MOV is utilized in determining the motor output torque and the limiting component.
IV. CALCULATION The following pages provide the calculation of the maximum bonnet pressure, in each case, the motor is the limiting thrust cornpar,ent. The resultant bonnet pressure is back-calculated based on this limit from the Comed methodology.
+
, FORM APF 05040102, REV. 00 CALC NO. _XX M440_,_
CALCULATION SHEET , .,o, ,
I SHEET _3_ OF _33_
ORIGINATOR: ,%fg DATE: y,p.g VERIFIED BY:
g DATE:ygg EJHV8811 A " ' !
INPUTS:
Reference
[ N/A ] Bonnet Pressure Pbonnet ===> 256 psi ' k (Back-Calculated)
[ M ] Upstream Pressure Pup ===> 46 psi '
(Would be similar for DP on EJHV8811 A)
[ N/A ] Downstream Pressure Pdown ===> 0 psi (Conservative DP value)
[ Att. B ] Disk Thickness t ===> 2.56 inches
[ Att. B ] Seat Radius a ===> 6.332 inches STN
[ Att. B ] Effective Hub Radius b ===> 2.560 inches yf([%
[ Att. B ] Hub Length L ===> 0.890 inches j [ K ] Seat Angle theta ===> 7 degrees pC 1 [ K ] Stem Diameter Dstem ===> 2.00 inches 44 D
[ B ] Poisson's Ratio v ===> 0.3
[ B ] Modulus of Elast. E ===> 27,600,000
[ L ] Static Pullout Force Fpo ===> 12,000 lbs 'S
[ N/A ] DP DP ===> 0 psi
[ N/A ] Line Pressure Closed LPc ===> 0 psi
[ N/A ] Lino Pressure Open LPo ===> 0 psi
[ N/A ] 010 DP Thrust 010 ===> 0 lbs I
[ N/A ] Open DP Run Load Fpk ===> 0 lbs l
[ M ] MotorCapability . OT ===> 22,567 lbs
[ M ] Max Allow Open Thrust MASTO ===> 45,000 lbs CALCULATED VALUES D ===> 4.240E+07 lbs-in L11 ===> 0.004 Pforce ===> 2.457E+04 lbs G ===> 1.062E+07 L17 ===> 0.118 ystretch ===> 1.924E-05 inches C2 ===> 0.135 DPavg ===> 233.21373 psi yq ===> -2.715E-04 inches C3 ===> 0.022 Mrb ===> -2.499E+03 lbs ysw ===> -2.532E-07 in/(Ibs/in)
C8 ===> 0.707 Ob ===> 1.528E+03 lbs/in ybw ===> -5.159E-07 in/(Ibs/in)
C9 ===> 0.297 ybd ===> -1.516E-04 inches ycompr ===> 3.116E-08 in/(!bs/in)
L3 ===>0 Ksa ===> -0.292 yw ===> -8.003E-07 in/(Ibs/in)
L9 === > 0 ysq ===> -1.006E-04 inches Fs ===> 13,496 lbs VF ===> 0.000 (See Ref. P) Mu ===> 0.28 PRESSURE LOCKING LOADS L Fpiston ===> 805 lbs Fpreslock ===> 4,212 lbs Fvert ===> 7,160 lbs Fpo ===> 12,000 lbs Ftotal ===> = - Fpiston + Fvert + Fpreslock +F ===> 22,567 lbs RESULTS Motor Cap, ===> 22,567 lbs Ftotal ===> 22,567 lbs MAST ===> 45,000 MARGIN ===> 0 %
, l
+
FORM APF-05D40102. REY. 00 CALC NO. ,,,_,,XX M 640,,_
CALCULATION SHEET ,,w ,o, ,
SHEET ,,,,4,,,,, OF ,,,,,,33_
ORIGINATOR: ygQ DATE:
V 5 M VERIFIED BY: pg DATE: yg EJHV88'11B "
INPUTS Reference
[ N/A ] Bonnet Pressure Pbonnet ===> 245 psi ' & (Back-calculated)
[ M ) Upstream Pressure Pup ===> 46 psi
[ N/A ] Downstream Pressure Pdown ===> 0 psi (Conservative DP value)
[ Att. B ] Disk Thickness t ===> 2.56 inches
[ Att. B ] Seat Radius a ===> 6.332 inches y4
[ Att. B ] Effective Hub Radius b ===> 2.560 inches
[ Att. B ] Hub Length L ===> 0.890 inches '/ !
[ K ] Seat Angle theta ===> 7 degrees pg
[ K } Stem Diameter Dstem ===> 2.00 inches y4&
[ B } Poisson's Ratio y == => 0.3
[ B ] Modulus of Elast. E ===> 27,600,000
[ N ] Static Pullout Force Fpo ===> 15,000 lbs lg
[ N ] DP DP ===> 207 psi
[ O ] Line Pressure Closed LPc ===> 203 psi
[ O ] Line Pressure Open LPo ===> 1 psi
[ N ] 010 DP Thrust O10 ===> 7,114 lbs
[ N ] Open DP Run Load Fpk ===> 3,058 lbs
[ M ] Motor Capability OT ===> 22,567 lbs
[ M ] Max Allow Open Thrust MASTO ===> 45,000 lbs CALCULATED VALUES .
D ===> 4.240E+07 lbs-in L11 ===> 0.004 Pforce ===> 2.338E+04 lbs G ===> 1.062E+07 L17 ===> 0.118 ystretch ===> 1.831E-05 inches C2 ===> 0.135 DPavg ===> 221.8636 psi yq ===> -2.583E-04 inches C3 ===> 0.022 Mrb ===> -2.377E+03 lbs ysw ===> -2.532E-07 in/(Ibs/in)
- C8 ===> 0.707 Ob ===> 1.453E+03 lbs/in ybw ===> -5.159E-07 in/(Ibs/in)
C9 ===> 0.297 ybd ===> -1.442E-04 inches ycompr ===> 3.116E-08 in/(Ibs/in)
L3 ===>0 Ksa ===> -0.292 yw ===> -8.003E-07 in/(Ibs/in)
L9 ===> 0 ysq ===> -9.571E-05 inches Fs ===> 12,839 lbs VF ===> 0.180 Mu ===> 0.18 PRESSURE LOCKING LOADS-Fpiston ===> 769 lbs Fpreslock ===> 1,525 lbs Fvert ===> 6,811 los Fpo ===> 15,000 lbs Ftotal ===> = - Fpiston + Fvert + Fpreslock +F ===> 22,567 lbs
-RESULTS " -
l l
Motor Cap. ===> 22,567 lbs Flotal ===> 22,567 lbs MAST ===> 45,000 MARGIN ===> 0 %
FORM APF OSD-Oe102, REY. 00
+
CALC NO. _._XX M-040,,,_
CALCULATION SHEET ,,vi.,Ou 0 SHEET ,,,_S_ OF _33_
ORIGINATOR: ,%ft DATE: y.f,g VERIFIED BY: ( gj DATE:y/g
' ~
EJRV8840 INPUTS Reference
[ N/A ] Bonnet Pressure Pbonnet ===> 1,199 psi l g (Back-calculated)
[ A ] Upstream Pressure Pup ===> 233 psi
[ N/A ] Downstream Pressure Pdown ===> 0 psi (Conservative DP vane)
[ Att. B ] Disk Thickness t ===> 2.744 inches
[ Att. B ] Seat Radius a ===> 5.011 inches y i(
[ Att. B ] Effective Hub Radius
[ Att. B ] Hub Length b ===> 2.694 L ===> 0.820 inches inches gf/g
[ Att. B ] Seat Angle theta ===> 7 degrees #
[ Att. B ] Stem Diameter Dstem ===> 2.50 inches 4W
[ B ] Poisson's Ratio v ===> 0.3
[ B ] Modulus of Elast. E ===> 27,600,000
[ C ] Static Pullout Force Fpo ===> 36,784 lbs g
[ A ] DP DP ===> 225 psi
[ A ] Line Pressure Closed LPc ===> 233 psi
[ A ] Line Pressure Open LPo ===> 8 psi
[ C ] 010 DP Thrust 010 ===> 13,103 lbs
[ C ] Open DP Run Load Fpk ===> 5,795 lbs l
[ C ] Motor Capability OT ===> 77,764 lbs
[ D ] Max Allow Open Thrust MASTO ===> 120,000 lbs CALCULATED VALUES D ===> 5.222E+07 lbs-in L11 ===> 0.002 Pforce ===> 6.073E+04 lbs G ===> 1.062E+07 L17 ===> 0.079 ystretch ===> 3.957E-05 inches C2 ===> 0.088 DPavg ===> 1082.8379 psi yq ===> -2.702E-04 inches C3 ===> 0.012 Mrb ===> -3.919E+03 lbs ysw ===> -1.281E-07 in/(Ibs/in)
C8 ===> 0.751 Ob ===> 3.588E+03 lbs/in ybw ===> -9.546E-08 in/(Ibs/in)
C9 ===> 0.284 ybq ===> -8.214E-05 inches ycompr ===> 2.051E-08 in/(Ibs/in)
L3 ===> 0 Ksa ===> -0.159 yw ===> -2.441 E-07 in/(Ibs/in)
L9 ===> 0 ysq ===> -1.485E-04 inches Fs ===> 34,853 lbs VF ===> 0.474 Mu ===> 0.50
, PRESSURE LOCKING LOADS -
Fpiston ===> 5,887 lbs Fpreslock ===> 26,047 lbs Fvert ===> 20,820 lbs Fpo ===> 36,784 lbs Ftotal ===> = - Fpiston + Fvert + Fpreslock +F ===> 77,764 lbs
-RESULTS4 -
Motor Cap, ===> 77,764 lbs Ftotal ===> 77,764 lbs MAST ===> 120,000 MARGIN ===> 54 %
x-- - - . . . . - - . . - .-
+
, FORM APF 06040102. REV. 00 CALC NO. _,_XX-M-040,,,,,_,
CALCULATION SHEET esvis,ou si SHEET 5fs,. OF _33 ORIGINATOR: g f4g DATE: % 5.% VERIFIED BY: /hd. h'~ DATE: 4.f ih EJflV8B40 INPUTS Reference
~
[ N/A ] Bonnet P. essure Pbcnnet ===> 2,300 psi (Back-calculated)
[ A ] Upstream Pressure Pup ===> 233 psi l
[ N/A ] Downstream Pressure Pdown ===> 0 psi (Conservative DP value) l
[ Att. B ] Disk Thickness t ===> 2.744 inches
[ Att. B ] Seat Radius a ===> 5.011 inches
- This calculation evaluates the total
[ Att. B ] Effective Hub Radius b ===> 2.694 inches force required by the handwheel of the
[ Att. B ] Hub Length L ===> 0.820 inches actuator when in the manual mode of
[ Att. B ] Seat Angle theta ===> 7 degrees operation and not the electrical (motor)
[ Att. B ] Stem Diameter Dstem ===> 2.50 inches mode.
[ B ] Poisson's Ratio v ===> 0.3
[ B ] Modulus of Elast. E ===> 27,600,000 Nole: The handwheel torque required
[ C ] Static Pullout Force Fpo ===> 36,784 lbs to obtain 120,000 lbs of force is:
[ A ] DP DP ===> 225 psi
[ A ] Line Pressure Closed LPc ===> 233 psi ==> 342 ft-lbs with a stem COF of 0.15
[ A ] Line Pressure Open LPo ===> 8 psi
[ C ] 010 DP Thrust 010 ===> 13,103 lbs ==> 416 ft-lbs with a stem COF of 0.20
[ C ] Open DP Run Load Fpk ===> 5,795 lbs
[ C ] Motor Capability OT ===> 77,764 lbs (Maximum handwheel shaft torque is
[ D ] Max Allow Open Thrust MASTO ===> 120,000 lbs 493 ft-lbs per reference D.)
CALCULATED VALUES ~ .
D ===> 5.222E+07 lbs-in L11 ===> 0.002 Pforce ===> 1.225E+05 lbs G ===> 1.062E+07 L17 ===> 0.079 ystretch ===> 7.979E-05 inches C2 ===> 0.088 DPavg ===> 2183.5 psi yq ===> -5.448E-04 inches C3 ===> 0.012 Mrb ===> -7.903E+03 lbs ysw ===> -1.281 E-07 in/(Ibs/in)
C8 ===> 0.751 Ob ===> 7.235E+03 lbs/in ybw ===> -9.546E-08 in/(Ibs/in)
C9 ===> 0.284 ybq ===> -1.656E-04 inches ycompr ===> 2.051E-08 in/(Ibs/in)
L3 ===> 0 Ksa ===> -0.159 yw ===> -2.441 E-07 in/(Ibs/in)
L9 ===>0 ysq ===> -2.994E-04 inches Fs ===> 70,279 lbs VF ===> 0.474 Mu ===> 0.50 PRESSURE LOCKING LOADS; Fpiston ===> 11,290 lbs Fpreslock ===> 52,523 lbs Fvert ===> 41,983 lbs Fpo ===> 36,784 lbs Ftotal ===> = - Fpiston + Fvet + Fpreslock +F ===> 120,000 lbs RESULTS ,
Motor Cap. ===> 77,764 lbs Ftotal ===> 120,000 lbs
- MAST ===> 120,000 MARGIN ===> 0 %
! , FORM APF-06D-00102, REV. 00 t
CALC NO. _XX M-040_._
CALCULATION SHEET nsvision o SHEET _6_ OF _33_
ORIGINATOR: jg DATE: y.g .g VERIFIED BY: g DATE:yg/ j g EMHV8802A !
INPUTS I Reference
[ N/A ] Bonnet Pressure Pbonnet ===> 3,822 psi 'g (Back-calculated)
[ N/A ] Upstream Pressure Pup ===> 0 psi (Conservative DP value)
[ N/A ] Downstream Pressure Pdown ===> 0 psi (Conservative DP value)
[ Att. B ] Disk Thickness t ===> 1.010 inches
[ Att. B ] Seat Radius a ===> 2.006 inches gg ,
[ Att. B ] Effective Hub Radius
[ Att. B ] Hub Length b ===> 1.056 L ===> 0.610 inches inches gp
[ Att. B ] Seat Angle theta ===> 7 degrees g,,4 4-
[ Att. B ] Stem Diameter Dstem ===> 1.25 inches 'fN
[ B ] Poisson's Ratio v ===> 0.3
[ B ] Modulus of Elast. E ===> 27,600,000
[ E ] Static Pullout Force Fpo ===> 5,000 lbs &
[ N/A ] DP DP ===> 0 psi
[ N/A ] Line Pressure Closed LPc ===> 0 psi
[ N/A ] Line Pressure Open LPo ===> 0 psi
- Mu was determined based on the worst
[ N/A ] 010 DP Thrust O10 ===> 0 lbs case open coefficient for similar valves
[ N/A ] Open DP Run Load Fpk ===> 0 lbs that were DP tested. (Ref. G)
[ F ] Motor Capability OT ===> 13,606 lbs (EMHV8801 A/B & EMHV8803A/B)
! F ] Max Allow Open Thrust MASTO ===> 16,000 lbs CALCULATED VALUES D ===> 2.604E+06 lbs-in L11 ===> 0.002 Pforce ===> 3.493E+04 lbs G ===> 1.062E+07 L17 ===> 0.083 ystretch ===> 1.102E-04 inches 3
C2 ===> 0.092 DPavg ===> 3822.1525 psi yy ===> -5.157E-04 inches C3 ===> 0.013 Mrb ===> -2.346E+03 lbs ysw ===> -1.441E-07 in/(Ibs/in)
C8 ===> 0.747 Ob ===> 5.264E+03 lbs/in ybw ===> -1.323E-07 in/(Ibs/in)
C9 ===> 0.286 ybq ===> -1.643E-04 inches ycompr ===> 3.976E-08 in/(Ibs/in)
L3 ===>0 Ksa ===> -0.168 yw ===> -3.161E-07 in/(Ibs/in)
L9 ===>0 ysq ===> -2.412E-04 inches Fs ===> 20,565 lbs VF ===> 0.000
- Mu ===> 0.16 PRESSURE LOCKING LOADS:
Fpiston ===> 4,690 lbs Fpreslock ===> 1,519 lbs Fvert ===> 11,777 lbs Fpo ===> 5,000 lbs Ftotal ===> = - Fpiston + Fvert + Fpreslock +F ===> 13,606 lbs RESULTS Motor Cap. ===> 13,606 lbs Ftotal ===> 13,606 lbs MAST ===> 16,000 MARGIN ===> 0 %
e
+
FORM APF 060 00102. REY. 00 CALC NO. ,,_XX M-040,_,
CALCULATION SHEET ,,vi ,o, ,
SHEET _7_ OF _33_
ORIGINATOR: ,gg "
DATE: y,y,g VERIFIED BY: gj DATE:gg EMFIV8802B v INPUTS.
Reference
[ N/A ) Bonnet Pressure Pbonnet ===> 3,378 Back-calculated)
[ N/A ) Upstream Pressure Pup ===> 0 psi psi l g (Conservative
(
DP value)
[ N/A ) Downstream Pressure Pdown ===> 0 psi (Conservative DP value)
[ Att. B ] Disk Thickness t ===> 1.010 inches
[ Att. B ) Seat Radius a ===> 2.006 inches
[ Att. B ] Effective Hub Radius b ===> 1.056 L ===> 0.610 inches inches
@[%p
[ Att. B ] Hub Length
[ Att. B ] Seat Angle theta ===> 7 degrees
[ Att. B ] Stem Diameter Dstem ===> 1.25 inches
[ B ] Poisson's Ratio v ===> 0.3
[ B ] Modulus of Elast. E ===> 27,600,000
[ E ] Static Pullout Force Fpo ===> 6,000 lbs g
[ N/A ] DP DP ===> 0 psi
[ N/A ) Line Pressure Closed LPc ===> 0 psi
[ N/A ) Line Pressure Open LPo ===> 0 psi
- Mu was determined based on the worst
[ N/A ) 010 DP Thrust 010 ===> 0 lbs case open coefficient for similar valves
[ N/A ] Open DP Run Load Fpk ===> 0 lbs that were DP tested. (Ref. G)
[ F ] MotorCapability OT ===> 13,606 lbs (EMHV8801 A/B & EMHV8803A/B)
[ F ] Max Allow Open Thrust MASTO ===> 16,000 lbs CALCULATED VALUES -
D ===> 2.604E+06 lbs-in L11 ===> 0.002 Pforce ===> 3.087E+04 lbs G ===> 1.062E+07 L17 ===> 0.083 ystretch ===> 9.738E-05 inches C2 ===> 0.092 DPavg ===> 3378.026 psi yq ===> -4.558E-04 inches C3 ===> 0.013 Mrb ===> -2.073E+03 lbs ysw ===> -1.441E-07 in/(Ibs/in)
C8 ===> 0.747 Ob ===> 4.653E+03 lbs/in ybw ===> -1.323E-07 in/(Ibs/in)
C9 ===> 0.286 ybq ===> -1.452E-04 inches ycompr ===> 3.976E-08 in/(Ibs/in)
L3 ===> 0 Ksa ===> -0.168 yw ===> -3.161 E-07 in/(Ibs/in)
L9 ===> 0 ysq ===> -2.132E-04 inches Fs ===> 18,175 lbs VF ===> 0.000
- Mu ===> 0.16 PRESSURE LOCKING LOADS Fpiston ===> 4,145 lbs Fpreslock ===> 1,343 lbs Fvert ===> 10,409 lbs Fpo ===> 6,000 lbs Ftotal ===> = - Fpiston + Fvert + Fpreslock +F ===> 13,606 lbs RESULTS -
Motor Cap. ===> 13,606 lbs Flotal ===> 13,606 lbs MAST ===> 16,000 MARGIN ===> 0 %
ron u m - = . nsv.
CALC NO. __XX44-040,_
l l
CALCULATION SHEET ,,y,, , , ,
l sassi _a_ or _ss_
ORIGINATOR: b ,%[7 DATE: y.,r, pg, VERIFIED BY: g DATE: gg ENftV0001
- INPUTS 4 .
! Reference i
[ N/A ] Bonnet Pressure Pbonnet ===> 322 psi g Back-calculated) i [ N/A ] Upstream Pressure Pup ===> 0 psi (Conservative DP value)
(
[ N/A ] Downstream Pressure Pdown ===> 0 psi (Conservative DP value)
[ Att. C ] Disk Thickness t ===> 1.250 inches
[ Att. C ] Seat Radius a ===> 5.563 inches S7Il
[ Att. C ] Effective Hub Radius
[ Att. C ] Hub Length b ===> 1.813 L ===> 4.063 inches inches gy
[ S ] Seat Angle theta ===> 5 degrees (,eo
[ U ] Stem Diameter Dstem ===> 1.38 inches Wit-
[ B ] Poisson's Ratio y ===> 0.3
[ B ] Modulus of Elast. E ===> 27,600,000
[ R ] Static Pullout Force Fpo ===> 7,000 lbs lg
[ N/A ] DP DP ===> 0 psi
[ N/A ] Line Pressure Closed LPc ===> 0 psi
[ N/A ] Line Pressure Open LPo ===> 0 psi
[ N/A ] 010 DP Thrust 010 ===> 0 lbs
[ N/A ] Open DP Run Load Fpk ===> 0 lbs
[ S ] MotorCapability OT ===> 17,766 lbs
[ Q ] Max Allow Open Thrust MASTO ===> 24,920 lbs CALCULATED VALUES D ===> 4.936E+06 lbs-in L11 ===> 0.006 Pforce ===> 2.797E+04 lbs G ===> 1.062E+07 L17 ===> 0.142 ystretch ===> 1.994E-04 inches .
C2 ===> 0.164 DPavg ===> 321.87502 psi yq ===> -2.227E-03 inches )
C3 ===> 0.028 Mrb ===> -3.683E+03 lbs ysw ===> -5.641E-07 in/(Ibs/in) '
C8 ===> 0.687 Ob ===> 2.456E+03 lbs/in ybw ===> -4.343E-06 in/(Ibs/in)
C9 ===> 0.288 ybq ===> -1.724E-03 inches ycompr ===> 2.492E-07 in/(Ibs/in)
L3 ===> 0 Ksa ===> -0.405 yw ===> -5.156E-06 in/(Ibs/in)
L9 ===> 0 ysq ===> -3.037E-04 inches Fs ===> 15,096 lbs VF ===> 0.000 (See Ref. Q) Mu ===> 0.28 PRESSURE LOCKING LOADSn Fpiston ===> 478 lbs Fpreslock ===> 5,790 lbs Fvert ===> 5,454 lbs Fpo ===> 7,000 lbs Ftotal ===> = - Fpiston + Fvert
- Fpreslock +F ===> 17,766 lbs RESULTS: -
Motor Cap. ===> 17,766 lbs Ftotal ===> 17,766 lbs MAST ===> 24,920 MARGIN ===> 0 %
l .
FORM APF 060 00102, REV. 00 I
l CALC NO. __XX4 040_,,,
CALCULATION SHEET ,Evi.,o, ,
SHEET _9_ OF 33_,,,
ORIGINATOR- gh DATE: g.g, g VERIFIED BY:
gg DATE:ygg ENMVO(f07 / "
. INPUTS-
, Reference
[ N/A ] Bonnet Pressure Pbonnet ===> 382 psi l 6 (Back-calculated)
[ N/A ] Upstream Pressure Pup ===> 0 psi (Conservative DP value)
[ N/A ] Downstream Pressure Pdown ===> 0 psi (Conservative DP value)
[ Att. C ] Disk Thickness t ===> 1.250 inches
[ Att.C] Seat Radius a ===> 5.563 inches gy
[ Att. C ] Effective Hub Radius b ===> 1.813 inches /p
[ Att. C] Hub Length L ===> 4.063 inches 4
[ S ] Seat Angle theta ===> 5 degrees
[ U ] Stem Diameter Dstem ===> 1.38 inches @%95
[ B ] Poisson's Ratio v ===> 0.3
[ B ] Modulus of Elast. E ===> 27,600,000
[ T ] Static Pullout Force Fpo ===> 5,000 lbs &
[ N/A ] DP DP ===> 0 psi
[ N/A ] Line Pressure Closed LPc ===> 0 psi I
[ N/A ] Line Pressure Open LPo ===> 0 psi l
[ N/A ] 010 DP Thrust 010 ===> 0 lbs
[ N/A ] Open DP Run Load Fpk ===> 0 lbs
[ F ] MotorCapability OT ===> 17,766 lbs
[ Q ] Max Allow Open Thrust MASTO ===> 24,920 lbs j CALCULATED VALUES l D ===> 4.936E+06 lbs-in L11 ===> 0.000 Pforce ===> 3.316E+04 lbs l G ===> 1.062E+07 L17 ===> 0.142 ystretch ===> 2.365E-04 inches C2 ===> 0.164 DPavg ===> 381.66974 psi yq ===> -2.641 E-03 inches C3 ===> 0.028 Mrb ===> -4.368E+03 lbs ysw ===> -5.641E-07 in/(Ibs/in)
C8 ===> 0.687 Ob ===> 2.912E+03 lbs/in ybw ===> -4.343E-06 in/(ibs/in) j C9 ===> 0.288 ybq ===> -2.044E43 inches ycompr ===> 2.492E-07 in/(Ibs/in)
L3 ===> 0 Ksa ===> -0.405 yw ===> -5.156E-06 in/(Ibs/in)
L9 ===> 0 ysq ===> -3.601E-04 inches Fs ===> 17,900 lbs VF ===> 0.000 (See Ref. Q) Mu ===> 0.28 PRESSURE LOCKING LOADS-Fpiston ===> 567 lbs Fpreslock ===> 6,866 lbs Fvert ===> 6,467 lbs Fpo ===> 5,000 lbs Ftotal ===> = - Fpiston + Fvert + Fpreslock +F ===> 17,766 lbs RESULTS.
Motor Cap. ===> 17,766 lbs Ftotal ===> 17,766 lbs MAST ===> 24,920 MARGIN ===> 0 %
FORM APF 05D40102. REV.63 I
CALC NO. XX M CALCULATION SHEET - ,o, o SHEET 10 OF 33 V. RESULTS / CONCLtJSIONS in all cases, sufficient margin exists for each of the valves to accommodate the effects of pressure locking. Further margin also exists if the actual motor capabll ty is determined from the actual field tested stem cc#,c;dit of friction.
The resultant maximum bonnet pressures for the three valves are as follows:
Yalya Maximum Bonnet Pressure EJHV8811 A 256 psi EJHV88118 245 pel EJHV8840 1,199 pel (electric motor capability) 2,300 psi (manual handwheel capability) l EMHV8802A 3.822 psi EMHV8802B 3.378 psi l
ENHV0001 322 psi ENHV0007 382 psi
. VI. REFERENCES 4
A. Procedure TP-TS-112 Rev.0, EJHV8840 MOV DP Test B. Mark's Standard Handbook for Mechanical Engineers, Ninth Ed.
C. WR 05781-92 and VOTES test #4 (DP test) and test #7 (Static As-Left test)
D. Calculation EJ-M-011 Rev. 6
. E. WR 03220-94 and VOTES test #8 (Static As-Left test)
F. Calculation EM-M-016 Rev. 2 G. Calculation EM-M-017 Rev. 7 H. WR 03219-94 and VOTES test #8 (Static As-Left test) i
- 1. PIR 95-0313, Pressure Locking and Thermal Binding
. J. Letter WO 96-0023, Submsttal to the NRC Concoming Pressure Locking and Thermal Binding of WCGS
, Valves for Generic Letter 95-07 f
K. Drawing M-724-00696 L WR 05770-92 and VOTES test #5 (Static As-Left test)
M. Calculebon EJ-M-013 Rev. 4 l N. WR 05784-92 and VOTES test #3 & 4 (DP test) and WR 04959-94 test #3 (Static As-Left test)
O. Procedure TP-TS-96 Rev. O, EJHV8811B MOV DP Test J P. Calculation EJ-M-017 Rev. 2 Q. Calculation EN-M-011 Rev. 2 R. WR 03216-94 and VOTES test #4 (Static As-Left test) i S. Calculation EN-M-005 Rev. 3 T. WR 03215-94 and VOTES test #3 (Static An-Left test)
U. Drawing M-225-00006 V. STS PE-19E and STS PE-400 performed during Refuel Vill ,,,. g p W. Calculation EN-M-013 Rev.1, 3
, X. Calculaton EJ-M-019 Rev.1 Y. PIR 96-109P and the supporting operability evaluation per /J'28-001 h yfh t> V q.s %
- rTAI ~-
A- l
~
'PALC..0. XX~ M - oVO l REV o
- EHT_.lL.0F E i PRESSURE LOCKING TESTING AT COMMONWEALTH EDISON
! PURPOSE Comed has developed a MathCad model for predicting the thrust required to unseat an j MOV under pressure locking conditions. This modelis based on Roark's Equations for
- deflection of a plate with a central hub. The MathCad model is being applied to MOVs j which a Comed review determined to be potentially susceptible to pressure locking.
1 I The purpose of the Comed test program for pressure locking is two-fold. The test data is i being used to validate the Comed MathCad model for pressure, locking. In addition, the j testing is being performed to determine the whether pressure locking concerns ===ad=W with slow heat-up of fluid in the valve bonnet are justi6ed.
The Westinghouse Owners' Group has been supporting the Comed efforts by soliciting
- other utility involvement and by providing some funding for the setup and testing of valves .
at Comed facilities. ,
j RESULTS TO DATE f Comed has tested a 10" Crane valve and a 4" Westinghouse valve under pressure locking l conditions. The results of this testing are plotted on the attached sheets As can be seen i from these plots, the MathCad model has very accurately predicted the pressure locking l j unseating force. l 4
- In addition, Comed performed some bonnet Suid heat-up testing on the Westinghouse MOV. This testing showed a bonnet pressurization rate of only 0.4 psi per degree temperature rise. This result is similar to results obtained by Northeast Utilities in pressure i
! locking tests performed earlier this year. Pdor to this test, as much air as possible was removed from the valve bonnet by venting through the packing. No seat leakage and very i i
slight packing leakage were observed during the test. Based on this test data, Comed l l*'~'~
i believes that extraordinary measures (such at those taken by TVA during 1985 tests) must be taken to sufBdaaely remove air from the valve bonnet so that theoretical pressurization rates of 30 to 100 psi per degree temperature rise can be achieved. TVA had to shake its test valves from side to side prior to submerging them in a heated bath ofwater to get the
- measured pressurization rates of 20 to 24 psi per degree temperature rise. Such extraordinary measures are inconsistent with normal plant operations. Consequently, thermally induced pressure locking due to bonnet heat-up appears to represent a design j i concern rather than an im H=*e operability concern No bonnet fluid heat-up testing of the Crane 10" valve could be performed because slight seat leakage was sufHeient to preclude bonnet pressurization by the thermally i_@cd j pressure locking mechanism. This information also suggests that the thermally iscM 1 pressure locking concern should not be considered a common cause type of failure which l i
has a high probability ofoccurring.
i
l
! FUTURE TESTING PLANS Several utilities have expressed interest in participating in the Comed test program by supplying test valves or performing testing of their own. This includes Entergy (Grand Gulf), Arizona Public Service, and Carolina Power & Light. Entergy is currently preparing to perform tests on a Velan valve using the Comed test procedure. APS and CP&L are offering test valves to Comed. In addition, Anchor / Darling has agreed to provide Comed with a 6" double-disk gate valve for pressure locking testing. At this time, Comed is considering testing the valves listed belowe.rrin;; 0ctober/ November of tlas year:
8" Borg-Warner Flex Wedge Gate Valve from APS
-- 8" Westinghm Flex Wedge Gate Valve from CP&L 6" Anchor / Darling Flex Wedge Gate Valve from CP&L 6" Anchor / Darling Double-Disk Gste Valve from A/D ATTACGMT A CALC.NO. XX' PI - O WO REV oo SHT IL OF M i
illl11 I ll i lllll iilli! ,l 3e3@=0g r .
i mI g@sC4g a
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Measured Pressure induced Load a b h h h h h a
l i ATTACF. MENT - A C ALC. l'10. XX~f ~*W" -
REV 00 SHT lY OF 33 ,
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ih oE a
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, Measured Unseating Load ' ~~ ~ ~ ' ' "
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Crane 10" Valve Pressure Locking Test Results Additional Load (above static unseating)
Due to Bonnet Pressure e000 3sooo
.i o M y m 8 30000
- e 2 <C d E t- k y
- - , ; -s E 28a o ya o
- e ifs W a cc S
g 1
.3
.* 15000 E e 2
- s 10000 ;
e s000 e +
1 0
0 5000 10000 15000 20000 25000 30000 35000 40000 Predicted Load Due to Pressure I
- 1. ."
1
. t
. COMMONWEALTH EDISON COMPANY e
CALCULATION NO. NED M MSD.188 PROJECT NO. N/A PAGE NO. 4
- 1. PURPOSE / OBJECTIVE The purpose of this calculation is to available marging (MGC to Required Thrust to Open) for MOV 3-1501-22A which has been determined to be susceptible to the pressure locking phenomena. The MOV is installed in the Low Pressure Injection (LPCI) System at Dresden.
!!. METHODOLOGY AND ACCEPTANCE CRITERIA The methodology for calculating the thrust required to open the MOVs under the pressure locking scenario is based on the Reference 1,(Roark's) engineering handbook. His methodology has been previously applied by Comed iri'tiie'!4/ences 2 and 10 calculations. The methodology determines the total force required to open the valve under a pressure locking scenario by solving for the four components to this required force. The four components of the force are the Pressure Locking Component, the static unseating component, the piston effect component, and the " reverse piston effect" component. These components are determined using the following steps.
Pressure Locking Comoonent of Force Reauired to Ooen the Valve The valve disk is modeled as two plates attached at the center by a hub which is concentric with the valve disk. A plane of symmetry is assumed between the valve disks. His plane of symmetry is considered fixed in the analysis.
_ lPlane 4 . of p Symmetry W
H w -
Modeled As: -l "Symmetzy m -
REVISION NO. ,.
O ATTACHMENT A CALC. No. k X -M- on REV o o SHT l2 0F.
COMMONWEALTH EDISON COMPANY l CALCULATION NO. NED-Af-AfSD-l#8 PROJECT NO. N/A PAGE NO.5 l 1 The pressure force is assumed to act uniformly upon the inner surface of the disk between 1 the hub diameter and the outer disk diameter. The outer edge of the disk is r.ssumed to be ! unimpeded and allowed to deflect away from the pressure force. In addition, the disk hub is I allowed to stretch. The total displacement at the outer edge of the valve disk due to shear and bending and due to hub stretch are calculated using the reference 1 equations. h b nding 6 shear 4-4- 4= l p & 1
~
me me C "'> "umu _g _u S'hub stretch An evenly distributed force is assumed to act between the valve seat and the outer edge of the valve disk. This force acts to deflect the outer diameter of the valve disk inward and to compress the disk hub. The pressure force is reacted to by an increase in this contact force between the valve disk and seats. The valve body seats are conservatively assumed to be fixed. Herefore, the deflection due to the known pressure load must be balanced by the deflection due to the unknown seat load. He deflection due to the pressure force is first calculated. Den, the reference 1 equations are used to determine the contact force between the seat and disk which results in a deflection which is equal and opposite to the deflectior. due to the pressure force. ATTACHMENT A CALC.N0. VY #-0# REV o o SHT lf 0F 3E REVISION NO. O
COMMONWEALTH EDISON COMPANY CALCULATION NO. NED-M-MSD-188 PROJECT NO. N/A PAGE NO.6 The coefficient of friction between the seat and disk is determined tased on the open valve l factor from a DP test. The stem force required to overcome the contact load between the seat and disk which opposes the pressure force is equal to: (seat load) x [ (seat mu) cos(seat angle) - sin (seat angle)] x 2 (for two disk faces). Static Unsentinn Force The static unseating force represent the open packing load and pullout force due to wedging i of the valve disk during closure. These loads are superimposed on the loads due to the pressure forces which occur during pressure locking. The value for this load is based on ! static test data for the MOVs. Piston Effect The piston effect due to valve internal pressure exceeding outside pressure is calculated using the standard industry equation. This force assists movement of the valve stem in the open direction. ,, , , , , , Fm f,, = xD 2 x (Pw - P,,)
" Reverse Piston Effect"(F y d P bonnet The reverse piston effect is the term used in this calculation to refer to the pressure force acting downward against
> Qe valve disk. This force is equal to the differential pressure across the valve disk times the area of the valve disk 0,, ,, times the sine of the seat angle times 2 (for two disk faces). p p inlet outlet m ATTACauENT A CALC. i:0. XX- A1- O VO 'b d REV oo SHT li 0F 51 REVISION NO. O
. - . - .. - . _ . ~.. - - _. . ..
. TMMONWEALTH EDISON COMPANY
; CA'LCULATION NO. NED-M-MSD-Is# PROJECT NO. N/A PAGE NO.7 Total Force Reauired to Overcome Pressure Lockinz As mentioned previously, the total stem force (tension) required to overcome pressure locking is the sum of the four components discussed above. All of the terms are positive with the exception of the piston effect component.
1 Next the motor gearing capability available to overcome static unseating forces is determined j using the statically measured stem factor, the pullout efficiency, the temperature factor, and the i Comed motor test data (for breakdown torque and voltage factor). 4 1
< w
% x TempFactor x OAR x Efp x
- StemFactor 4
i i
- 1
- i i'
i 4 T i 1 .t 1 a N i j ATTACHMENT A CALC.NO. XY- M- DW
- REV 00 SHT zo 0F n REVISION NO. #
~
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a
_ _ . . __ __ _ _ ._ __ ._ _ _ . . _ . _ __ __~. COMMONWEALTH EDISON COMPANY CALCULATION NO. NED.M.MSD l## PROJECT NO. N/A PAGE NO. # ) I Determination of Onen Valve Factor Review of the VOTES traces for the subject MOV indicate a ~4000 lbf inconsistency between the - thrust zero at 04 (valve closed) and the thrust zero at C3 (valve opened). His is explained by j the valve's horizontal orientation. The weight of the valve stem when the valve is open is j putting a side load on the valve yoke causing the zero mismatch. L The open valve factor is calculated by based on the open DP load. His load is determined by l using the equation below: The 010 thrust is measured in the region of the trace during which
' the valve disk is sliding on the valve seat (prior to flow initiation). This thrust is based on the 4 04 zero since the valve is effectively closed at 010. The open running thrust is measured at the - end of the open stroke and is referenced to the C3 zero since the valve is nearly fully open at the point at which the open running load is measured. The Line Pressure adjustment term in the i equation accounts for the fact that the piston effect decreases during the opening valve stroke. ,
i ClO m -Runningw + D' (ClOw, - Runningw,)
%* DPxx D*
- 4 i
) The apparent margin between MGC and required thrust is calculated. No acceptance criteria is provided in this calculation. The Station will establish the acceptability of the available margin as part of the operability analysis for this valve. I j III. ASSUMPTIONS
- 1. He valve disk is assumed to act as two ideal disks connected by a hub. The
- o,' ,,, _ equations in reference I are assumed to conservatively model the actual load due to pressure forces. This assumption is considered conservative since inspection of the
~
- disk drawings show large fillets between the disk hub and seats which should make the valve disk stiffer than assumed in the reference 1 equations.
i i ATTAcil'l2IT A cal.C. NO. U-hoV8 REV
- o SHT_ALOF O
REVISION NO. 0
.- COMMONWEALTH EDISON COMPANY I
i CALCULATION NO. NE:D M-MSD-188 . PROJECT NO. N/A PAGE NO.9 l l i
- 2. De coefficient of friction between the valve seat and disk is assumed to be the same !
under pressure locking conditions as it is under DP conditions. This assumption (in combination w .h assumption 2) is considered to be justified based on bench marking of the calculation against Comed and EPRI pressure locking test data for similar flex-wedge gate valves.
- 3. The upstream, downstream, and bonne: pressure values are based on a scenario in which the valve bonnet is pressurized to reactor pressure by leakage past adjacent check valves. A LOCA occurs which causes the reactor pressure drop off a rate defined in the applicable fuel analysis. The LPCI and LPCS pumps come up to speed, and the subject valves receive a signal to open. He pressure values are based on a review of the fuel analysis and FSAR for each station. These values should be reviewed by the affected stations for accuracy prior to final teceptance of this calculation. (See LIMITATIONS at end of this calculation.)
IV. DESIGN INPUTS l
- 1. Valve Disk Geometry information is based on the Reference 4 Fax from Crane Valve l Company (Attachment 1) l
- 2. Motor Data is taken from the Reference 5 report.
V. REFERENCES
- 1. Sixth Edition of Roark's Formulas for Stress and Strain
- 2. MPR Calculations 101-013-1, "Effect of Bonnet Pressure on Disc to Seat Contact Load", dated 3/23/95; and 101-013-4, " Estimate of Valve Unseating Force as '
Function of Bonnet Pressure", dated 3/23/95
- 3. NMAC Report NP-6660 D, " Application Guide For Motor Operated Valves" I hTTACHMNT A CALC.h3. X M -DVD REV o o SHT_2.E 0FM REVISION NO. O L______________-_ ___ _ _____ _ _ _ _ _ . _ - _ - - - _ .
COMMONWEALTH EDISON COMPANY 1 ~ CALCULATION NO. NED-M-MSD-188 PROJECT NO. N/A PAGE NO.10 i
- 4. Crane Telecopies from Dave Dwyer and Bruce Harry to Brian Bunte (Comed) dated 5/3/95 and 6/16/95, Attachment 1
- 5. Comed MOV AC Motor Test Program Report Part 1, Revision 1, CHRON 213741
- 6. EMS Calculation CE-DR 030, " Pressure Locking Analysis of Dresden Motor j Operated Valves", dated 6/13/95
- 7. Comed AC Induction Motor Test Report, Part 1, Chron 213741 dated April 27,1995 a
- 8. nrust values are taken from the following static and DP VOTES tests:
Station Y.alyg Test Number (s) Test Date A. Dresden 3-1501-22A 40 7/6/94 B. Dresden 3-1501-22A 42 7/6/94 3
- 9. Margin Review Databases for Dresden Station (dated 11/11/94)
- 10. Comed Calculation NED M MSD-182," Verification of Operability for Dresden and
{ ! Quad Cities Injection Valves Susceptible to Pressure Locking", dated June 22,1995 t.
- - VI CALCULATIONS ,
1 j MathCad calculation of: 1
- 1) the pressure locking unseating force,
- 2) the available motor gearing capability to unseat while pressure locked i is provided on the next 4 pages.
? I i b n: TAC; M NT A CALC.H0. XW-M-91p REV o o SHT E__OF 33 9 REVISION No. # l 'f s
4 4 9 EXAMPLE INPUTS: Pbonnet = 1005 psi Bonnet Pressure Assumption 5 Upstream Pressure P up = 380 ps.i Assumption 5 Downstream Pro,ssure p don = 350 psi Assumption 5 Disk Thickness =3in Attachment 1 Seat Radius a .= 6.385 in Reference 9 Hub Radius b .= 2.125 in Attachment 1 Hub Length L =2.4375 in Attachment 1 Seat Angle b := 54g Reference 9 Poisson's Ratio (disk) '3 Typical of Carbon Steel Mod.of Elast.(disk) E = 27.610$ psi Typical of Carbon Steel Static Pullout Force F po = 36921 Ibf Reference 88 (Test 42) 010 Thrust (DP test) 010 := 10048 lbf g,g,,,,,, gg Open Run Thrust (DP) Run .= 2268 lbf g,, ,, gg DP DPtest . . ,8 5 pp, . . Reference 8A LPelose .= 302.6 psi LP (valve closed) , LP (valve open) If0 Pen .= 45.6 psi Stem Diameter D stem .= 3 in geforence 9 VALVE FACTOR CALCULATION Valve Factor: (010 - Run) + " D mem (LPelose- LPopen)
*(a)2 DPtest Coefficient of friction between oisk and seat:(Reference 3) mu := VF-
# mu = 0.274 1 - VF sin (theta)
PRESSURE FORCE CALCULATIONS i Average DP across disks: l P up tP% DPavg =640 psi l DPavs := Pbonnet - 2 I l 1 i
\
1 M TACH;..a <T A CALC. l;0. XY- M- PV P BEV UoSHT21.0F W
o Disk Stiffness Constants (Reference 1, Table 24) D= Ed D -6.824107 lbfin 2 12-(I - v ) G: 0 = 1.06210' psi 2-(l + v) Geometry Factors: (Reference 1. Table 24) r ,3 ! I fb32 f 3 C I ' ! l + 2 in , C 2 = 0.161 2 :4- ga; i (bu , I Jl 2 2 l b b3 fa t fb C 3.=-4a
- - , +1 In +1 - -1 C 3 = 0.028 at (bj (a f'bl 2' l 3
C g =0.689 C g := 2 1 + v + (1 - v) (St i C9 I- I*'in_{- a 1-v g,[pI* I C 9 = 0.29 a 2 bj 4 \at , a ft2 a f ,3 f,12 L3.-- '-l+1 In +1 - 1-I L3=0 4a , (at (at (at 2" L9 f + I I L9=0 i f 32 ' ' b32 ft' b 2 r In: ,3' L g g : 64-1+4.b -5'bl*l l 2+1 - Lg i = 0.006 a rt rt a tag (at rbi , I i i - 1 1-v 1-bi' - fb3 2' 1 + ( I + v) In f ,3 L g7 =0.139 1 L 37. 4 (b;, 4 (Si tat Moment (Reference 1, Table 24, Case 2L) M g .= ~
**8 ' "
Cg
---(a-b)-L
,2 a b
' 2 2 17 Mtb --9.381 103 lbf 1
2 2 Q b: 2b -(a - b ) Qb= 5.45910' b m
' ATTACHMSJT A CALC.NO. Eh Ni- W 6 l REV o o SHT F OF 31 l
9*
5 e Deflection due to pressure and bending (Reference 1. Table 24, Case 2L) DPavg af ~ ybq:Mrb- C 2+Q. b C 3- L y q = -4.138 10 ' in Deflection due to pressure and shear stress:(Reference 1, Table 25, Case 2L) I f f b32 '
- K , = . 0.3- 2In .)1-1+!
- - K , --0.393 tjb (at K , DPavg s* _ ; y sq : y ,q = -3.223 10 ' in i Deflection due to hub stretch (from center of hub to disk):
4 2 2 P ro,,, = 3.1416 (a - b ) DPavg Pg =7.28910 lbf ] 4 P force L , 4 y stretch - 2 y stretch = 2.269 10 in
- 3. 4 6 b (2 E) 1 Total Deflection due to pressure forces:
yq :y bq + Y sq - Y swetch Y q =-9.629 10 *in Deflection due to seat contact force and shear stress (per ibfilr(Reference 1, Table 25,
- Case 1L)
-1.2- Iq a ,
y ,, = -2.647 10 ~7 - '" i- y,w:- 7 I (per Ibflin)
\ai
! Deflection due to seet contact force and bending (per Ibflin(Reference 1, Table 24, i f 3) fC) 2 fa C9) 't i
*'.**"6~ y bw - -L9 -
C3 +L3 y bw = -4.608 10-7
,lbfi iD (per Ibflin)j -(C gj
'i bj 'l\b.
3 (m1 . Deflection due to hub compression (per Ibflin),(from center of hub to disk): 2aa L g y 2 Y compr = 1.249 10 , ' (perIbflin) 3.1416 b (2 E) , (is j I Total deflection due to seat contact force (per Ibf//in.):
~7 -
Y w ::Y bw + Y sw - Y compr Y w = -8.504 10 l (per Ibflin) g ATTACH.'UNT A > CALC.N0. XW/Pl- 0W REV eo SHT_26 0F 31
+. 'o ,
l
. in . !
Seet Contact Force for which deflection is equal previously calculated deflection l from pressure forces: F,=2a-ab F , = 4.543 10' lbf l Yw UNSEATING FORCES i F% s included in measured static pullout Force l 3 F p;, goo = " D stem P% ... ,- . F piston = 7.104 10 lbf Fvert :s a sin (theta)-(2 Pbonnet- Pup - Pdown) Fvert = 1.42910' lbf l Fplock .: 2 F ,.(mu-cos(theta) - sin (theta)) Fpreslock = 1.69210' lbf F og,i :-Fpi.ston + Fvert + Fpreslock + Fpo F po = 3.692 10' Ibf Ftotal =6.10310' lbf MOTOR / GEARING CAPABILITY INPUTS: Motor Torque: MR 88.2 it Ibf Reference 9 Temperature Factor: Tf :: 0.98 Reference 9 Degraded Voltage: DV 402 volt Reference 9 under Voltage Factor: n 2.187 Reference 5 (Typical) Stem Factor: SF .: .0275 it Reference 9 . Overall Ratio: OAR = 48.45 Reference 9 Pullout Efficiency: Reference 9 Effpo = 0.65 CALCULATIONS: f oy e
'# II' MGC ,y i;, = 7.372 10' lbf MGC ,y ig, = MR Tf OAR Eff po-MGC ,y,;g, - F total Margm. .: Margin = 0.208 Ftotal
! TTACHMENT A
ALC. N0.
, XW M-0VP l AEV 00 SHT 27 0F 31
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3 M a k y B $ Cele- XY.-M.-O'{0 Py 18 e$31 ~ o fR o o) (
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O (o Westin0 house $%3,3 m Electric Corporation SM96-100 v
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A February 5,1996 7 f4 -66RM Mr. Lanny Ratzlaff WolfCreek Nuclear Operating Corp P. O. Box 411 Burlington, KS 66839 !
Subject:
Geometric Parametersfor Valve Pressure Locking Analysis _ J
Dear Mr. Ratzlaff:
In response to your recent request, this letter transmits geometric parameters for several Westinghouse valves. These geometric parameters are for use in the pressure locking analysis of these valves, using the Commonwealth Edison methodology, being done by Wolf Creek to support their response. The geometric parameters which we are providing are as follows: Star Angle: The value provided is one half of the angle between the two (2) faces of the disc, from the gate disc drawing. For all of these valves, the seat angle is 7 degrees. l Stem Dla*titt: This is the stem diameter where the stem passes through the packing. ! l Hub Radius: When the hub is circular, the hub radius is the hub radius from the gate disc drawing. When the hub is non-circular, the hub radius is the radius of a circle which has the same area as the actual hub. H ub Lenerk: The hub length is the distance between the two (2) disc flanges at the bottom of the wedge, it is recognized that this may give a larger hub length than is actually present in the hub itself, but this is the dimension used in the Commonwealth Edison analysis of the Westinghouse 4" gate valve which was used to verify their technique against test results. Disc Thickness. The value reponed is equal to the wedge thickness at mid-height of the wedge as given on the gate disc dmwing, minus the hub length defined above, quantity divided by 2. This disc thickness is actually the thickness of the disk at its outside edge at mid-height of the wedge, and as with the hub length dimension, this is the value used in the Commonwealth Edison calculation for the Westinghouse 4" gate valve which was used to validate the model.
+' ff:.dwy 6 h Csl5 XX -M - 010 fy 11 J 3%
b, . l O I m j O \ O Mr. Lanny Ratzlaff February 5,1996 b) Wolf Creek Nuclear Operating Corp Page Two (2) l
\
0 y
\ :
A 1 T 4 Seat Radias: The values given are the mem seat mdius as given by the following formula: seat radius = square root of[(OD squared plus ID squared)/8] The outside seat diameter used in this formula is the outside diameter of the seat area given on the seat ring dawing. The inside seat diameter is taken as the avemge of the inside seat diameter from the seat ring drawing and the inside seat diameter from the seat ring drawing divided by the cosine of 7 degrees. The outside seat diameter is given in the plane of the seat, while the inside seat diameter is given in the vertical direction. The inside of the seat ring is actually thus an ellipse, and we are using the average diameter of the ellipse. The table of values is attached. Very truly yours, WESTINGHOUSE ELECTRIC CORPORATION i 1 (
. h M. C. Bollenbach Special Sales Representative North American Field Sales MCB: sis ATTACHMENT cc: Mr. Carl Dumsday (W) WCNOC Site l
l 1 . 1
j Ag. L 4 B 6 CA. je x -m - oyo Ap 3. J n y . o . o O PJ '
\ TABLE OF VALUES o
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D i 7 VALVE GPOASSY VAL VEID TA G No. SERIAL NE!MBER DRA WING 4GM78FNA 8802A 04000GM88FNB0D000W750008 9749D75 4GM78FNA 8802B 04000GM88FNB0D000W7500ll 9749D75 10GM78FNC 8840 10000GM88FNB0D005W750006 9747D09 12GM88SEF 8702A 12002GM88SEH0F000W750002 3D21943 , 12GM88SEB 8702B 12002GM88SEH0D000W750004 3D21499 14GM84 FED 8811 A 14000GM84FEH0E005W750001 ID99954 14GM84 FED 8811B 14000GM84FEH0E005W750002 ID99954 l DISK SEA T HUB HUB SEA T DIAMETER THICKNESS RADIUS RADIUS LENGTH ANGLE STEM TA G No. L inches htChtE inches inChts detites inches 8802A 1.01 2.006 1.056 0.61 7 1.25 88028 1.01 2.006 1.056 0.61 7 1.25 8840 2.744 5.011 2.694 0.82 7 2.50 8702A 3.225 5.987 3.225 1.31 7 3.00 8702B 3.225 5.987 3.225 1.31 7 3.00 88 IIA 2.560 6.332 2.56 0.89 7 2.00 8811B 2.560 6.332 2.56 0.89 7 2.00 i
ID: FEE 08',9 15,:10 No.03 1 01 fNCHORDARLING 0 40 #4/9 st//cim t C 6 dc. M-M-oYo O Wy Il rh II (PE COtAT TELECOPIER NUMBER 3 /d .3 6 4 1 0f[ DATE A 6 TO: / Ass'M b. R 4 7~,2 L W F NUMBER OF PAGES / PLUS INSTRUCTON SHEET = E
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MESSAGE FROM / [ M M M 8-- ANCHOR /DARLJNQ VALVE COMPANY WILLIAMSPORT, PENNSYLVANIA Four Solutions To Problems ,,,, N ,,,, With Small Valves! ~ 9 Size % * . 2'
^ . ASME lil Class 1,2,3 (From Stock) e GreP hite Peoking i . Carbon or Stainless I
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ANCHOR / DARLING VALVE CO. WILLIAMSPORT, PA 17701
- Tel: 717-327 4800 Telex: 759953 FAX: 717 327-4805 I
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.Ei DISK SEAT HUB HUB VALVE # THICKNESS DIAMETER DIAMETER LENGTH e
r ENHV0001 i '4. 4 r ** **- 41 +r '2 da" " ENHV0007 i '4 5 "' ' 11.125 3.625 3'+ 'r 4 " *'"" l pg -p N All dimensions are in inches.
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'. Atta:hmentg t3 C:Ic. XX-M-C40, R/0 i W t/i'/[9 6 ! Independent venfication of the inputs and outputs for EMHV88028 found on sheet 5 of this calc. l!
! Inputs:
1 Sonnet Pressure Pbonnet = 4,269 psi 5 rm. L4se Peng,yy, 7y33 Upstr:am Pressure Pup = 0 psi r_,m g'*0M __ vasti F->cw z.,g 7, Pdown = 0 psi ~"' Downstream Pressure l Disk Thickness t= 1.010 in j SIst Radius a= 2.006 in Effectiva Hub Radius b= 1.056 in C ap w yyI g M 8d447 ) l j Hub Length L= 0.610 in d 5 E.o Ia 7,,.g g gE l
- Seat Angle theta = 7 deg '415
, St:m Diameter Dstem = 1.25 in c A L < u L 4TJoa, y= 0.3 l Poisson's Ratio 3 g. ,, f =
Modulus of Elast. E= 27.600,000 psi /T Static Pullout Force Fpo = 3,993 lbs DP DP = 0 psi
- Line Pr:ssure Closed LPc = 0 psi Line Pressure Open LPo = 0 psi 010 DP Thrust 010 = 0 lbs I Open DR Run Load Fpk = 0 lbs
- Motor Capability OT = 13,606 lbs Max Allow Open Thrust MASTO = 16,000 lbs !
1 1 Cf -_ ^ ' _ ^* Vagues:: om . - sw + s :>,. < > . eum r.w > a r unsen l D= 2604057 !bs-in L11 = 0.002 Pforce = 39013 lbs G= 10615385 L17 = 0.083 ystretch = 1.231E-04 in l C2 = 0.092 DPavg = 4269 psi yq = -0.000576 in C3 = 0.013 Mrb = -2620 lbs ysw = -1.44E-07 in^2/lb C8 = 0.747 Qb = 5880 lbs/iri ybw = -1.32E-07 in^2/lb l ! C9 = 0.286 ybd = -0.000184 in ycompr = 3.976E 08 in^2/lb l 2 L3 = 0 Ksa = -0.168 yw = -3.16E-07 in^2/lb l L9 = 0 ysq = -0.000269 Fs = 22969 lbs i VF = 0.000 Mu = 0.16 1 Pressure Locking Loads: < a. w w , a ' Fpiston = 5239lbs Fpreslock = 1697 lbs Fvert = 13154 lbs Fpo = 3993lbs i Flotal= 13605 lbs i Results: # , m m <m Motor Cap = 13606 lbs Ftotal= 13605 lbs MAST = 16000 lbs i l Margin = 7E.46 % l The re:ults of this verification agrees with those on sheet 5. Therefore, the results on sheet 5 are correct. 33 D Page.lWbfp u t. :-<v fs
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- n. , a v 1 WESTINGHOUSE ELECTMC CORPORAT10N SysTuMs a MAJOR PROJECTS MWSION/MSE COVER SHEET FOR TELECOPY NO. (412) 374-6639 WIN: 284-6639 Attention: / A Jun fbrusW Leontkn:
rw No.: 3 / 6 -3 4. Y- 7'o f f Car &menian No.: .. Netss: g ) ,) i L As M ad $ p g ,4 y ; p o)q , b la M7W? W b' d A do < /% & . I i l i i From: j 'Mald9 Phone: 6 </O I Dete: l */$ff'[ Telecopy No.: (412) 374 6630 w WIN 284 6639 or WIN 204 6647 i i NUMBER OF PAGES (haiveths cover sheet) 2*
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- 94-05-1990 15s14 I~TA64MIEgf '{ # 7,
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l fl* 1 *&1 PAGE 2 OF 2 l
! VEVE - L.0@i78FNC ! DWG - 9747D09 QUESTION: WHAT IS THE BASIS OF THE MAXIMUM OPEEATING LOAD OF i 112084 LE FOR THE VALVE AND CAN THE VEVE WI".'ESTAND AN OPENING l
LOAD OF 120,000 LE IF REQUIRED. l BASIS FOR CONCLUSION: i
! THE ELONAELE OPENING LOAD OF 112084 LB WAS BASED ON THE VEVE
- LINK AT 650F. THIS VEUE WAS BASED ON AN ELOWABLE OF .65 Sy AT l NEICE WESTINGHOUSE GENERELY USES FOR AS-LIFT CONDITIONS. '
$ LOWER TEMPERATURES THE LOADS NOULD EE: ; 600F - 113676 LE i 500F - 116616 LE ' 400F - 120414 LB 4 EL THESE VEURS ARE EASED ON THE SAME ELOWAELE AS THE 112004 LB. ! PLEASE NOTE THAT THE OPEEATING LOAD APPLIED TO THE STEN IS NOT 1 i THE LOAD ON THE INTERNAL COMPONENTS SINCE SOME OF THE LOAD IS
- USED TO PULL THE STEN THROUGH THE PACKING.
1 l ALL THE OTHER COMPONENTS AS LINK, PIN, STEM AND DISC CAN TAKE OPENING IDADS GREATER THAN 150,000 LB. i ,' CONCLUSION: i THE VEVE WOULD BE ACCEPTABLE WITH A 120,000 LB OPENING LOAD BASED 05 TEE ELOWAELE STRESS (.65 Sy) , THE FACT THE TEMPEEATURE , i WOULD NOT BE AT 650F AND THE FACT THAT THE PACKING LOADS WOULD l REDUCI THE LOADS ON THE LINK. I e 1}}