Text

Rev 1 to A10.1-AD-003, Pressure Locking Evaluation of Movs.
	ML18040A362
Person / Time
Site:	Nine Mile Point
Issue date:	10/21/1997
From:	Cruz D; NIAGARA MOHAWK POWER CORP.
To:	;
Shared Package
ML17059C644	List: ML17059C643; ML18040A362;
References
	A10.1-AD-003, A10.1-AD-003-R01, A10.1-AD-3, A10.1-AD-3-R1, NUDOCS 9904300086
	Download: ML18040A362 (305)
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{{#Wiki_filter:(Enclosure 1 consists of Calculation No. A10.1-AD-003, titled "Pressure Locking Evaluation of MOVs." Enclosure 1 has 137 pages, which are numbered from 1 to E4)

0 GARA Page 1 ( Next Z ) U MOHAWK ~CA'LC.UL'AT:.lON.',C,OV;ER'SHEET".,"" Tetai /s7 NUCLEAR ENGINEERING Last C'4 NINE MILE POINT NUCLEAR STATION Unit (1, 2 or 0=Both): 2 Discipline: MECHANICAL Title Calculation No. PRESSURE LOCKING EVALUATIONOF MOV'S A10.1-AD-003 (Sub)system(s) Building Floor Elev. Index No. VARIOUS NA NA NA Originator(s) DOMINGO A CRUZ Checker(s) I Approver(s)

                          ~. A l    e  (K ldll/Cg IC. Ze tee Design          Prep'd Rev                   Descri tion             'han     e No.        B             Date        Chk          Date         A             Date 01            COMPLETE REVISION TO               NA                 DAc a         8-25-yg INCORPORATE DISP.

00A AND TO USE MOST CURRENT INDUSTRY INF. Computer Output/Microfilm Filed Separately (Yes / No / NA): NO '.: Safety Class (SR / NSR I Qxx): SR Superseded Document(s): A10.1-AD@03, REV. 00, . ~+c</I /e(9', e DOCument CrOSS ReferenCe(S) - FOr additianal referenCeS See page(S):46NE 'b<C.O )titsrS % tg. ~ & eg4bO 4- G Ref Doc Document No. T e Index Sheet Rev SEE SECTION 4.0 General Reference(s): NONE Remarks: NONE Confirmation Required (Yes / No): No Final Issue Status File Location Operations Acceptance See Page(s): NA ( APP I FIO/ VOI ): APP ( Cele I Hold ): Gale Required ( Yes I No ): No Evaluation Number(s) I Revision: NA Component ID(s) (As shown ln MEL):

                                                 /                     2CSH'MOV101,2CSL'MOV107,2ICS         MOV121,122,128,129,2RHS'MOV Copy of Applicability      Review  Attached (Yes    N/R)7NR 115,116,4A,B,C,2SWP'MOV17A,B,1 8A,B,21 A,B,66A,B,67A,B,94A,B Key Words: PRESS LOCKING, GL89-10, MOV THRUST, SR, MECH, NMP2, GL95%7
'gl'gl04300086 9'gI042i                                                                                           ¹ FORMAT NEP-DES-08, Rev. 02 (F01)

PDR ADQCK 050004i0 P PDR

GARR::::! e': '-'!:.::: '-': ':: ': '::.: -f-: .::" Page 1 ( Next Ia 7 P l CALCULATIONCOVER SHEET Total NUOLEAR ENGINEERING NINE MILE POINT NUCLEAR STATION Unit (1, 2 or 0=Both): 2 Disci pline: MECHANICAL Title Calculation No. PRESSURE LOCKING EVALUATIONOF MOV'S A10.1-AD-003 (Sub)system(s) Building Floor Elev. Index No. VARIOUS NA NA NA Originator(s) DOMINGO A. CRUZ A ('(~ Checker(s) / Approver(s)

@~i~r~ S.Z~~,~

Design Prep'd Rev Descri tion Chan e No. B Date Chk Date A Date 01 COMPLETE REVISION TO NA Dhce tll-25-yg INCORPORATE DISP. 00A AND TO USE MOST CURRENT INDUSTRY INF. Computer Output/Microfilm Filed Separately (Yes / No / NA): NO . Safety Class (SR I NSR I Qxx): SR Superseded Document(s): A10.1&D403, REV. 00, . ts+~I //6/pg Document Cross Reference(s) - For additional references see page(s):4QNE ><Ca lild'rS % 8, < G acket>"r i. + Ref Doc Document No. T Index Sheet Rev SEE SECTION 4.0 General Reference(s): NONE Remarks: NONE Confirmation Required (Yes / No): No Final Issue Status File Location Operations Acceptance See Page(s): NA (APP I FIO I VOI ): APP ( Cele/ Hold ): Cele Required ( Yes / No ): No Evaluation Number(s) I Revision: NA Component ID(s) (As shown in MEL): Copy of Applicability Review Attached (Yes I N/R)? NR 2CSH'MOV101,2CSL'MOV107,2ICS'MOV121,122,128,129,2RHS'MOV 115,116,4A,B,C,2SWP'MOV17A,B,18A,841 A,B,66A,B,67A,B,94A,B Key Words: PRESS LOCKING, GL89-10, MOV THRUST, SR, MECH, NMP2, GL95%7

                                                                                                                      ¹ FORMAT NEP-DES48, Rev. 02 (FOI)

       %NIAGARA N U MOHAWK                        CAL'CULATION'CONTINUATIONSHEET                                  Page
                                                                                                   <@ext ra NUCLEAR ENGINEERING                                               v Nine Mile Point Nuclear Station                   Unit: 2                                Disposition:  NA Originator/Date 3c ef.

rn ow A.C,~ // 8/Ls'/rg ~ Checker/Date JP.JH7 A10.1-AD-003 Revision 01

1.0 PURPOSE

The purpose of this evaluation is to assess the capability of various motor operated valves to open against potential pressure locking conditions as described in NUREG 1275, Operating Feedback Report - Pressure Locking and Thermal Binding of Gate Valves, and to address GL89-10, Supplement 6 and GL95-07. The following valves have been identified as potentially susceptible to pressure locking per NER-2M-007, Rev. 1, "Pressure Locking I Thermal Binding of Safety Related Power Operated Valves". This evaluation uses the current design basis to determine the acceptability of these valves.

2.0 SCOPE

High Pressure Core Spray System - 2CSH'MOV101 Low Pressure Core Spray System - 2CSL MOV107 Reactor Core Isolation Cooling System - 2ICS'MOV121, 2ICS" MOV1 22, 2ICS*MOV128 and 2ICS'MOV129 Residual Heat Removal System - 2RHS'MOV115, 2RHS'MOV116, 2RHS*MOV4A, 2RHS*MOV4B and 2RHS'MOV4C Service Water System - 2SWP*MOV17A, 2SWP'MOV17B, 2SWP'MOV1 8A, 2SWP'MOV18B, 2SWP"MOV21A, 2SWP'MOV21B, 2SWP'MOV66A, 2SWP'MOV66B, 2SWP*MOV67A. 2SWP'MOV67B, 2SWP'MOV94A and 2SWP MOV94B I

3.0 METHODOLOGY

For each of the valve groups, the most limiting pressure locking j conditions will be identified. Utilizing the formulas derived from the Commonwealth Edison the required thrust to open the valve subject to pressure locking is determined (Ref. ,'ethod, and adjusted with the Kalsi Engineering Enhanced Pressure Locking Methodology (Ref. 31). '),

4.0 REFERENCES

I NOTES:

1. NMPC Telecon with Anchor Darling, dated 8l22l95, (Attachment A)

'.

MPR-1691, "Nine Mile Point Unit 2 Gate Valve Pressure Locking Due to Bonnet Heatup", dated November 1995

3. Limitorque Manual, NMPC File No. N2L20000VALVE003, Rev. 0., and EPRI Application Guide to MOVs, Doc. No. NP-6660-D, Section 3.3.3.

FORMAT ¹ NEP-DES-08, Rev. 01 (F02)

V NIAGARA N 4 MOHAWK NUCLEAR ENGINEERING CALCULATIONCONTINUATION SHEET Nine Mile Point Nuclear Stat/on Unit: 2 Disposition: NA Originator/Date ef.

      ,,. 4,. C.n  ~letzshg               ~

Checker/Date

                                                    /o-/H7      A10.1-AD-003 Rension 01

4. Velan Report DM-0050, page A4, (Attachment 8)

5. NUREG I CP-0152, page 3C-9 through 3C-34, "Commonwealth Edison Company Pressure

            ,Locking Test Report", (Attachment C)

6. NUREG I CR-5807, page 5 through 11, "Improvement in Motor Operated Gate Valve Design and Prediction Models for Nuclear Power Plant Systems" (Attachment D)

7. For 2CSH'MOV101 DBR-CSH-MOV101, Rev. 1, and MOV sizing calculation No. A10.1-G-048, Rev. 0

8. For 2CSL MOV107 DBR-CSL-MOV107, Rev. 1, and MOV sizing calculation No. A10.1-F-032, Rev. 0

9. For 2ICS MOV121 DBR-ICS-MOV121, Rev. 2, and MOV sizing calculation No. A10.1-H-059, Rev. 0

10. For 2ICS MOV122 DBR-ICS-MOV122, Rev. 2, and MOV sizing calculation No. A10.1-H-059, Rev. 0

11. For 2ICS'MOV128 DBR-ICS-MOV128, Rev. 2, and MOV sizing calculation No. A10.1-H-059, Rev. 0

12. For 2ICS'MOV129 DBR-ICS-MOV129, Rev. 2, and MOV sizing calculation No. A10.1-H-059, Rev. 0

13. For 2RHS*MOV4A DBR-RHS-MOV4A, Rev. 1, and MOV sizing calculation No. A10.1-E-139, Rev. 0

14. For RHS'MOV48 DBR-RHS-MOV48, Rev. 1, and MOV sizing calculation No. A10.1-E-139, Rev. 0

15. For 2RHS MOV4C FORMAT ¹ NEP-DES-OS, Rev. 01 (F02)

Y NIAGARA 0 MOHAWK NUCLEAR ENG1NEERING CAL'CULATIONCONTINUATION SHEET Page (Next ~S 4 Nine Mile Point Nuclear Station Unit: 2 Disposition: NA Originator/Date Checker/Date Revision Qv m'en<.c A,. C-aux /8/Zt A7 /0 ./4'~ A10.1-AD-003 01 ef. DBR-RHS-MOV4C, Rev. 1, and MOY sizing calculation No. A10,1-E-139, Rev. 0

16. For 2RHS" MOV115 DBR-RHS-MOV115, Rev. 1, and MOV sizing calculation No. A10.1-E-139, Rev. 0

17. For 2RHS" MOV116 DBR-RHS-MOV116, Rev. 1, and MOV sizing calculation No. A10.1-E-139, Rev. 0

18. For 2SWP*MOV17A DBR-SWP-MOV17A, Rev. 1, and MOV sizing calculation No. A10.1-N408, Rev, 0

19. For 2SWP'MOV17A DBR-SWP-MOV17A, Rev. 1, and MOV sizing calculation No. A10.1-N408, Rev. 0

20. For 2SWP"MOV18A DBR-SWP-MOV18A, Rev. 1, and MOV sizing calculation No. A10.1-N408, Rev. 0

21. For 2SWP'MOV18B DBR-SWP-MOV18B, Rev. 1, and MOV sizing calculation No. A10.1-N408, Rev. 0

22. For 2SWP'MOV21A DBR-SWP-MOV21A, Rev. 1, and MOV sizing calculation No. A10.1-N408, Rev. 0

23. For 2SWP'MOV21B t e DBR-SWP-MOV21B, Rev. 1, and MOV sizing calculation No. A10.1-N408, Rev. 0

24. For 2SWP'MOV66A DBR-SWP-MOV66A, Rev. 1, and MOV sizing calculation No. A10.1-N408, Rev. 0

25. For 2SWP'MOV66B DBR-SWP-MOV66B, Rev. 1, and MOV sizing calculation No. A10.1-N408, Rev. 0 FORMAT ¹ NEP-DES-08, Rev. 01 (F02)

V NAGARA N U MOHAWK NUCLEAR ENGINEERING CALCULATIONCONTINUATIONSHEET Page (Next ~ee Nine Mile Point Nuclear Station Unit: 2 Disposition: NA Originator/Date DC')e) >'l )e, i> I ~ C. Recta / 8/2C /5'7 Checker/Da y -/rt/-f7 A10.1-AD-003 Revision 01 ef.

26. For SWP*MOV67A DBR-SWP-MOV67A, Rev. 1, and MOV sizing calculation No. A10.1-N408, Rev. 0 2?. For 2SWP'MOV678 DBR-SWP-MOV678, Rev. 1, and MOV sizing calculation No. A10.1-NQ08, Rev. 0

28. For 2SWP'MOV94A DBR-SWP-MOV94A, Rev. 1, and MOV sizing calculation No. A10.1-N408, Rev. 0

29. For 2SWP'MOV948 DBR-SWP-MOV948, Rev. 1, and MOV sizing calculation No. A10.1-N408, Rev. 0

30. Roark's Formulas for Stress and Strain, Sixth Edition 1989, pages 398,399,404,405,408.409 444 and 445, (Attachment E)

31. ENHANCED PRESSURE LOCKING METHODOLOGY, Kalsi Engineering, inc. (1997) 5.0 CALCULATION RESULTS: As documented as the bottom of the last page for each valve evaluated, the thrust margin is either positive or negative. A positive thrust margin indicates that the valve and actuator is likely to overcome applicable theoretical pressure locking phenomena. A negative thrust margin indicates that the valve and actuator may not be able to overcome the applicable theoretical locking phenomena. Of the valves evaluated, valves 2CSH'MOV101, 2CSL MOV107, 2ICS'MOV121, 2ICS MOV129, 2RHS'MOV115, 2RHS MOV116, 2RHS'MOV4A, 2RHS'MOV48) 2RHS MOV4C) 2SWP'MOV21A, 2SWP'MOV218, 2SWP*MOV66A, x

2SWP'MOV668, 2SWP'MOV678 and 2SWP'MOV948 yielded a negative thrust margin. However, an evaluation of plant configuration, normal and accident, and system function for each of the valves analytically susceptible to pressure locking indicates no operability concerns and the valves will operate under postulated accident scenarious. A detail evaluation of the results of this calculation for the valves identified as susceptible to pressure locking phenomena is included in NER-2M07, Rev. 02. CHECKERS NOTE: This calculation was hand checked, therefore the MATHCAD commonly used commercial program does not required validation for this application. FORMAT ¹ NEP-DES-08, Rev. 01 (F02)

Niagara Mohawk Power Corporation Nuctear Engineering NMP 2 Calculation Cont. Sheet Page Qt /37 A10.1-AtM03, Rev. 01 Origina torl Date Checker/Date o harms y ~ a. C w ~/,s/y> Valve ID no: 2CSH'MOV101 Re uired 0 enin Force Deternmination under Pressure Lockin Conditions COINED Method DESIGN INPUTS: Design Basis Conditions at time of Pressure Locking Event: Upstream pressure (psig), P>.=55 Valve Bonnet pressure (psig), Pboggct 2477 ryP. Downstream pressure (psig), Pdo~' 4 II Valve Disk Geometry: r hub radius, b:=2 mean seat radius, a:=6.125 average disk thickness, t:= 1.66 hub length, L:=0.094 seat angle, a:= 6 e:=-'" e =o.o52 2 180 Valve Disk Material Properties: e is half disk anglect modulus of elasticity, E:=29400000 Poisson's Ratio, v:=0.3 Other Valve Parameters: Valve Stem Diameter, D ~.-- LS Static Unseating Thrust, F ~'.=4385 ( reference: Test ¹ 8, 4/18/96 ) Valve Factor VF:= 0.5 ( reference: NER-2M410 ) CALCULATIONS: cope) Coefficient of friction between disk and seat, It'.=

                                                                     '- a~(e)         It =0.513    ( reference ¹6 )

P~+Pdo~ gives,'P AverageDPAcrossDisk, DPavg Pbo~<- avg 2 45'10 2 Disk StNnes Constants, D:= Et and G:= E 12 1-v 2 (1+v) which gives, D 1.232 10 and G =1.131 ~ 10 Geometry Factors, C2 '.=-1 1-4 I+2 ln C3 '= + I In + 1 C8.'=- 1+v+(1 1 2 v) b a C 9.--b a 1-1+v ln 2 a b

1-v 4 b a 2 which gives, C2 0.164 C 3 =0.028 C8 0'68 C 9 =0.289 COMED PL Evaluation Valve ID: 2CSH'MOV1 01 page 1 PCSH101A.MCD

I Niagara Mohawk Power Corporation NMP 2 Page fo( t S t Nuciear Engineering Calculation Cont. Sheet A1 0.1-AD403, Rev. 01 Onginatorloate Checker/Date o~ ~)~ 4-<~ ~~tnhq Additional Geometry Factors, . fp'=b 2 4 2 2 I fp fp 4 fp fp In-I+4 5 2+ ~ 64 a a a a rp L17.=- I -I 4

I-U I - 4 a 0 4

a 0 2

I+(I+Y) In a fp

which gives, L I I =0.006 and L17 ~0/141 Moment Factors, 2 M fb'= DPavg'a C9 /2

                                                     '0)2                            ob:=       '"'(*- 0*)

C8 2ab 2b which gives, Mfb =-3.389 10 and Q b ~2.052'10 Deflection from pressure/bending, 3 4 2+ Q b C 3 - a a avga y bq:=M fb' L 11 D D D which gives, yb q ~i).008 Deflection from pressure I shear, 2 2 K ~:=-0.3 2 In a I + rp I-2 rp in-b ysq'= m'DP avg a b a which gives, K sa &.404 and y ~%.002 Deflection from pressure I hub stretch,

                                                                                       -P fotee L
                                -b
                        '=

ofee tt (a ) DP avg y stretch

                                                                                     'tb     2E which gives,                 P fo~ =2.579. 10               and        y ~      =-3.281 ~ 10 COMED PL Evaluation                                 Valve ID: 2CSH'MOV1 01                                              page 2 PCS H101A.MCD

I 0

Niagara Mohawk Power Corporation NMP 2 Page ~of (3 I Nuorear Engineering Celcutation Cont. Sheet A1 0.1-AD403, Rev. 01 Onginatorloate Checkerloate ~~a+> k~ C C4>4 <(tet l~r) Q Io I-r< Total Deflection due to pressure, yq:=ybq+ysq+yg t h which gives, yq =<.OI Additional Geometry Factors r0'.= a L3 '.=ro 4.a ro a 2

                             + I In   +a ro ro -

a 2 I ro L9,= I+v In a

2

                                                                                        + I-v a

ro 4 1-ro a 2 which gives, L3 ~0 and L9=0 P Deflection from seat load/bending, w:= I y bw'.= O C2 ro C9 CS b L9 ro C3 b

                                                          + L3      which gives,          ybw                2317    10 6

Deflection from seat load I shear, Ksa:=-1.2 ro ro

a In- b y ~:= Ksa tG which gives, Ksa -1.343 y~ ~-4.383 10 Deflection from seat load I hub compression, L

                        -2 tta    2 y'ompr    'tb                    which gives,               ycom r Total Deflection from unit seat load, y w:=ybw+ysw+ycompr                        which gives,             yw     2'76 10 contact load distribution,                                                10'quilibrium w equilibrium '=

yq ~hi~h gi~es, 3.517 wequilibn~ yw Load per seat = 2.tt a yq =1.354 I0 yw Pressure Locking Force, COMED PL Evaluation Valve ID: 2CSH'MOV101 page 3 PCSH101A.MCD

Niagara Mohatttrk Power orporatton NMP 2 Page 1 o(/37 Nuciear Engineering Catctglation Cont. Sheet A10.1-AD403, Rev. 01 Checker/Date gag ///-(0< Fpres lock:= 2m a

Yq

                                   'PM<e)-      sm(e)) 2           which glvm. Fpres lock=1245'los Jw Piston Effect Force,                        P  an',=0 piston    streettem '[       bonnet       ann)          which gives,    F;   1   ff t =4.377'10 "Reverse Piston Effect" Force, F vert  .'= (t a  2 P bonnet up     down      'sin(0)          which gives,     F ~ = 3.022  10 Total Force R        ulred to Overcome Pressure Lockln "total   'res      lock+ "po+ vert        piston effect F to~       1'546805 ACTUATOR CAPABILITY:

Actuator Model ISize: = SMB-00-10 Motor Torque Output: TQm:= 9.3 tt- lbs Gear Ratio: OGR:=72 Application Factor. Af:=0.9 Pullout Efficienc: Eff:=0.4 Reduced Voltage: RV:= 1.0 Torque Output: TQout:= TQm RV .OGR.Af Eff TQout ~ 241.056 tt- lbs Stem Factor. Thrust Capability: THcap: = TQout Sf Sf:= 0.018919 THcap =1.274 10 lbs NOTE: RV IS SQUARE IF ACTUATORIS AC. ENHANCED PRESSURE LOCIQNG METHODOLOGY: KEI:= 1.20 a Thrust Margin:= THeap (p tomt KEI) Thrust Margin ~ -1.729'10 lbs

Conclusion:

Open Thrust Margin is negative, therefore this valve and actuator are unlikely to overcome the theoretical pressure locking conditions evaluated. COMED PL Evaluation Valve ID: 2CSH'MOV1 01 page 4 PCSH101A.MCD

Niagara Mohawk Power Corporation Nucteer Engineering NMP 2 Calcutation Cont Sheet Page /OH /+7

A1 0.1-AD403, R et/. 01 w e~ ~/i~bp Originator/Date Checker/Date

                                                                     >-i17 Valve ID no: 2CSL'MOV107 Re uired        0     enin    Force Deternmination under Pressure Lockin Conditions COMED Method DESIGN INPUTS:

Design Basis Conditions at time of Pressure Locking Event: Upstream pressure (psig), Pp.=500 Valve Bonnet pressure(psig), Pboggat =8931 Downstream pressure (psig) P dp~ Disk Geometry: 'alve hub radius, b:=1.25 mean seat radius, a:= 1.879 average disk thickness, t:=0.626 hub length, L:=0.25 seat angle, a:= lo e:=-a tt 2 180 e =0.087 Valve Disk Material Properties: e is half disk anglea modulus of elasticity, E:=29400000 Poisson's Ratio, v.=0.3 Other Valve Parameters: Valve Stem Diameter, D <~.'=1.375 Static Unseating Thr'ust, Fpo 3399

¹

( reference: Test 4, 6/3/96 ) ( reference: NER-2M410 ) CALCULATIONS:

                                                                           ~ge)

Coefficient of friction between disk and seat, It:=

                                                                        '- sa(e)             It =0.521    ( reference ¹6 )

Pup+Pdo~ Average DP Across Disk, DP avg:=P bomct- gives DP avg 8 681 1(P 2 Disk Stittnas Constants, D:= Et and G:= E l2 t-v 2 2 (I+ v) which gives, D =6.605 10 and G =1.131 ~ 10 Geometry Factors, C2.=-I 4 I-b

a I+2 In a b C3'.=. b 4a b

a I In a b

b a I C8.'=-I 2 I+v+(I-v) b a 2 C a

9.--b I+v ln 2 a b

I v 4 I b a 2 which gives, C2 0.049 C3 0.005 C 8 =0.805 C 9 =0.241 COMED PL Evaluation Valve ID: 2CSL MOV107 page 1 PCSL1 07A.MCD

Niagara Mohawk Power CorPorat/on NMP 2 Page /r of /p7 Nuclear Engineering Calculation Cont. Sheet A10.1-AD403, Rw. 01 Originate rloate Qcwr~ g 4 @Ace C Jr P/$ 7 ~ Checker/Date

                                                                                 ~-i-17 Additional Geometry Factors,                                      rp  .'=b 2              4                2                2 I

I+4 rp 5 rp 4 rp 2+ rp In- a 64 a a a rp L17 4 I I- I-v 4 I- rp a 4 rp a 2

I+(I+v) ln-rp which gives, L I I =4.463 10 and L i7 =0.046 Moment Factors, 2 Mrb '=- DP avg a C9 a -rp -L17 '"'(*- 0') C8 2ab 2b which gives, Mrb -2.113 10 and Qb 6.834-10 Deflection from pressure/bending, 4 a y b '.=M rb.C 2+ Q b - a C avg L 11 D D 3 D which gh/es, yb q ~-2.798'10 Defiectlon from pressure I shear, 2 2 K:=-0.3 a 2 in I+ b

rp ~ I 21n- rp b sa t.G avg a a which gives, K sa =%.077 and y sq =-3.348'10 Deflet%ion from pressure I hub stretch,

                                                                                             -P force L Pf        lt (a       b ) DP g                        ystretch-ttb 2E which gives,                 P f0~0 =5.368.10
                                                                             -

and y ~~ -4.649 10 COMED PL Evaluation Valve ID: 2CSL MOV107 page 2 PCSL1 07A.MCD 4

0 Niagara MotunNk Power Corporation NMP 2 Page/2d /ST Nuclear Engineering Calculation Cont. Sheet A A10.1-AD403, Rev. 01 Originator/Date Checker/Date Qo~p~ A.C~P r /ralph ~ ~-<7 Total Deflection due to pressure, yq y bq+ y sq+ y stretch which gives, y q =<.611 ~ 10 Additional Geometry Factors r:=a L3 = ro

4-a ro a 2

                                + I ln   +  - I a

ro ro a 2 ro L9.I+v In a

2

                                                                                             + I-v I-a ro      4 ro a

2 which gives, L3 0 and L9 ~0 Deflection from seat load I bending, w:= I II ybw. O C2 roC9 CS b L9 .

                                                   - roC3' b
                                                                 + L3      which gives,         bw =-1.458 10 Deflection from seat load I shear, Ksa '=-1.2     In-                      y ~!=Ksa-       a which gives,          Ksa   <.489 a        b                              tG y sw =-1.298'10 Deflection from seat load I hub compression,                         '

L 2'll'a h y compr "'= which gives, y compr 1023 10 ttb E Total Deflection from unit seat load, yw:=ybw+ysw+ycompr which gives, yw -2.85810 Equilibrium contact load distribution, w equilibrium ' yq which gives, w equilibrium ~ Load per seat= 2 tt a yq yw

2.731 ~ 10 4 Pressure Locking Force, COMED PL Evaluation Valve ID: 2CSL MOV107 page 3 PCSL1 07A.MCD

8 4 l

Niagara Mohawk Power Corporation NMP 2 Pat/e/> of r 3bT Nigciesr Enpineeriny Calculation Cont. Sheet A10.1-ADO03, Rev. 01 Onpinstor/Date Checker/Date 4 C esc> //tike!r gr

                                                                      /)./i)/4 F

p ] k 2 n a (it

                                 'Yq cos(e) sin(0)) 2           which g/vesa    F W

Piston Effect Force, P a~."=0 2 piston street ' stem '( bonnet atm) which ganesa Fp,ston cffcct =1326'10 "Reverse Piston Effect" Force, 2 vmt [s'e '( 'onnet deum)j'smigi which gives, F v~ = 1.678'10 up Total Force Re uired to Overcome Pressure Lockin F total l=F pres lock+ F po + F'vert- F'piston cffcct which gives F total 3 049697 10 ACTUATOR CAPABILITY: Actuator Motor/Size: = SMB-00S-15 Motor Torque Output: TQm:= 14.18 ft- lbs Gear Ratio: OGR:= 23 Application Factor: Af:=0.9 Pullout Efficiency: Eff .s= 0.45 Reduced Voltage: RV: = 0.8848 Torque Output TQout: = TQI RV OGR AfEff TQout = 103.407 ft- lbs Stem Factor: Sf': = 0.017861 TQout Thrust Capability: THcap:= 'IHcap 5.79 10 1bs Sf NOTE: RV IS SQUARE IF ACTUATORIS AC. ENHANCED PRESSURE LOCNNG METHODOLOGY: KEI:= 1.20 Thrust Margin:= THoap '(pmmt KEI) e Thrust Margin -3.081 ~ 10 lbs

== Conclusion:== Open Thrust Margin is negative, therefore this valve and actuator are unlikely to overcome the theoretical pressure locking conditions evaluated. COMED PL Evaluation Valve ID: 2CSL'MOV107 page 4 PCSL107A.MCD

Niagara Mohawk Power Corporation NMP 2 Page/Q/I'3 7 Nuclear Engineering Calculation Cont. Sheet A10.1-AtM03, Rev. 01 Originator/Date 6/itlF7 W v-i~7 Checker/Date Valve IDno: 2ICS MOV121 Re uired 0 enin Force Deternmination under Pressure Lockin Conditions COMED Method DESIGN INPlJTS'esign Basis Conditions at time of Pressure Locking Event: Upstream pressure (psig), P>> ..= 1200 Valve Bonnet pressure (psig), P bonnet 1200 Downstream pressure (psig), P down 0 Valve Disk Geometry: hub radius, b:= 3.063 mean seat radius, a.'=4.45 average disk thickness, t:=1.012 hub length, L:=0.188 seat angle, u.=10 6:=-a rt 2 180 0 0.087 Valve Disk Material Properties: e ishalfdiskangle a modulus of elasticity, E:=29400000 Poisson's Ratio, v:=0.3 Other Valve Parameters: Valve Stem Diameter, D< .=2.5 Static Unseating Thrust, F>>.=27694

                                                                                 ¹ (raference: Test 7, 1/9/96)

Valve Factor VF:=0.6 (reference: NER-2M-010) CALCULATIONS: Coefficient of fnction between disk and seat, lt:= ~ge)

                                                                                 - sin(e)            It = 0.631     (reference   ¹ 6) up~     down Average DP Across Disk,                           avg  'onnet                   2 glvesr      DP avg     600 Disk Stitfnes Constants,                    D:=       Et             and         G:=       E 12(i-')                              2 (1+v) which gives,                  D =2.79   10          and           G = 1.131 ~ 10 GeometryFactors,                     C2'.=-I 4

I- b

a I+2 1n a b

C3.'= b 4a b

a I In a b b

                                                                                                                    +  - I a

C8.'= I 2 I + v+(I - v) b a C a I-9.--b I+v In 2 a b

I-v 4 b a 2 which gives, C2 0.043 C 3 =0.004 C8 0.816 C 9 =0.23 COMED PL Evaluation Valve ID: 2ICS MOV121 page 1 PICS121A.MCD

n Niagara Mohawk Power Corgoration NMP 2 Pager+o//P7 Nuclear Engin<<ring Catcutation Cont. Sh<<t A10.1-AD403, Rev. 01 Originator/Date Checker/Date Wa~ 4.C~~ ~/rPl~ czf85 >-i r7 Add/t/onal Geometry'actors, rp =b 2 4 2 2 fp fp fp rp I I+4 5 -4 2+ ln- a 64 a a a a rp L17.=- I 4 I- I-v 4 I- a 0 4

                                             -     fp

a 2 I+(I+v) In a rp which gives, L I I ~3.398 10 and L17 =0.04 Moment Factors, 2 DP avg a 9 DP avg M rb.'=- a -rp -L17 Qb.'= (a ro j C8 2ab 2b which gives, M rb -698.979 and Qb 1.021'10 Deflection from pressurelbend/ng, 4 avg a yb .'=M*C2+Qb C3-a a D D D LII which gives, yb q -1.078 10 Deflection fmm pressure/sheer, 2 2 K sa .'=-0.3 2 In a

                                     - I+     rp      ~

I - 2 In-rp sa'vg a b a b ysq which gives, K sa ~%.066 end y ~ =W.877'10 Deflecflon from pressure /hub stretch, P fofoo'L force '=tt (a

                                 - b ) DP avg                             ystretch-ttb 2E which gives,              P f             1.964-10           end        y ~t,>    -2.131 ~ 10 COMED PL Evaluation                                Valve ID: 2ICS'MOV121                                               page 2 PICS121A.MCD

f Niagara Mohawk Power CorPoratlon NMP 2 Page Aaf /3P

Nuclear Engineertng Calculation Cont. Sheet A1 0.1-AD403, Rev. 01 originator/Date Checker/Date Qc~r~ rg. Q~p ~-i-e7 Total Deflection due to pressure, yq ' bq+ -" sq + y stretch which gives, y q =-1.787 10 Additional Geometry Factors ro,'=a L3 .'= ro

4a ro a 2

                                +1    ln +

a ro ro a 2

                                                        -1            L9     .

a

ro lyv a 2 ln + ro 1-v 4 III 1-ro a 2

        'bw    '9 Ksa: =- 1.2 a3.w D

which gives, Deflection from seat load/bending, ro ro

a C2 C8 Deflection from seat load/shear, ln- b ro.C 9 b y sw L3 0

roC3 i=Ksa b w:=1 a tG

                                                              + L3 and which g/ves, which gives, L9    0 ybw ~-3.67 Ksa  -0.448 10 y ~ ~ -1.743'10 Deflection from seat load/hub compression, L
                          -2 tta 2 y compr '=                          which gives,               y         =-3.033    10 ttb Total Deflection from unit seat load, yw:=ybw+ysw+ ycompr                            which gives,            y      -5.443 10 Equilibrium contact load distribution, yq equilibrium   'w              which gives,         weq~brium 328415 Load per seat =           2 tt a yq     9.183 1(P yw Pressure Locking Force, COMED PL Evaluation                               Valve ID: 2ICS'MOV121                                               page 3 PICS121A.MCD

Niagara Mohawk Povtter Corporation NMP 2 Pager 7of /P7 N uctear Engineering Catculation Cont. Sheet A10.1-AD403. Rev. 01 Originator/Date Checker/Date @capri@ A ~ C.~/ tr/Z5ly7 IO.W P Fp~ lock'tt'a (Itcos(8)- Yq

                                 ~'w sin(0)) 2         whichgives,      Fpr     s lock  9938 10 Piston EN'ect Force,                           P  au:=0 piston street
                        '

stem '( bonnet, stm) F 1st "Reverse Piston Effect" Force, F crt.= rt a 2pbonnct down wh/ch g/ves F ycrt 6 506 I 0 up Total Force Re uired to Overcome Pressure Lockin F <<taI:=F pres lock+ F po+ F ycrt- F piston affec which gives, . F <<~ = 3.824814 10 ACTUATOR CAPABILITY: Actuator Model ISizer = SB-2-60 Motor Torque Output: TQm:= 51.63 ft- Ibs Gear Ratio: OGR:= 101.52 Application Factor: Af:=0.9 Pullout Efficiency: EK:=0.35 Reduced Voltage: RV:= 0.8627 Torque Output: TQout: = TQm RV OGR AfEff TQout ~ 1.229'10 ft- Ibs Stem Factor: Sf: = 0.029481 TQout Thrust Capability: THcap:= THcap ~4.168 10 lbs SE NOTE: RV IS SQUARE IF ACTUATOR IS AC. ENHANCED PRESSURE LOCIQNG METHODOLOGY: KEI:= 1.20 Tbtnst Mssipn:= THeep (F tomt KEI) Thrust Margin ~-4.216 10 Ibs

Conclusion:

Open, Thrust Margin is negative, therefore this valve and actuator are likely to overcome the theoretical pressure locking conditions evaluated. COMED PL Evaluation Valve ID: 2ICS MOV121 page 4 PICS121A.MCD

Niagara Mohawk Power Corporation NMP 2 Page/got /'37 Nuclear Engineering Calculation Cont. Sheet A10.1-AD403, Rev. 01 Originator/Date Checker/Date Durga A ~ C49 t )pljrr Valve ID no: 2ICS MOV122 Re uired 0 enin Force Deternmination under Pressure Lockin Conditions COMED Method DESIGN INPUTS'esign Basis Conditions at time of Pressure Locking Event: Upstream pressure (psig), P>> .= 160 Valve Bonnet pressure (psig), P bonnet,.=160 Downstream pressure (psig), P d .=0 Valve Disk Geometry: hub radius, b:=4.94 mean seat radius, a = 5.75 average disk thickness, t:=0.789 seat angle, a:=7 e:=- a tt 2 180 e =o.o61 Valve Disk Material Properties: e ishalfdiskangle a modulus of elasticity, E:=29400000 Poisson's Ratio, v:=0.3 Other Valve Parameters: Valve Stem Diameter, D ~.=2 Static Unseating Thrust F po 9730

                                                                            ¹ (reference: Test 30, 10/27/93)

Valve Factor VF:=0.5 (reference: NER-2M-010) CALCULATIONS:

                                                                          ~ge)

Coefficient of friction between disk and seat, it:=

                                                                      '- ~(e)                     lt = 0.515   (referece   ¹6) up+ down Average DP Across Disk,                  DP       'bonnet                                  gives,       DP avg,   80 avg                            2 Disk Stiffnes Constants, Et 3           and         G.        E 12    1-v                             2 (1+v) which gives,            D =1.322   10          and          G =1.131 ~ 10 Geometry Factors,              C 2.'=  1+ 2 ln                        C 3 '.= +               1  ln  +   .  -  1 C8.=- 1+

1 2

b a 2 C 9.-- 1- ln + which gives, C2 0.009 C 3 =4.316'10 C 8 =0.908 C 9 =0.124 COMED PL Evaluation Valve ID: 2ICS MOV122 page 1 PICS122A.MCD

0 h Niagara Mohawk Power Corporation NMP 2 Page /fol ~T Nuctear Engineering Calculation Cont. Sheet A10.1-AD403, RW. 01 Originator/Date Checker/Date +~~ ~ Ai O~y 4 /jpl+T 7-1+7 Additional Geometry Factors, rp.=b hh 2 4 2 I I+4 -5 -4 0 0 0 2 1- rp In- a 64 a a a a rp L17 I 4 I- "4 I-U I -' a 4

a 0 2 I+(I+Y) In rp a which gives, L I I =1.545 10 and L 17 0.009 Moment Factors, 2 DP avg a C9 Mrb '=- a -rp -L17 '( 0) C8 2ab 2b

             'hich gives, Mrb -28.505                 and             Q b =70.113 Deflection from pressurelbending, 4
                                 '=Mrb C2+Qb' C3-                               avg a                   a yb D                   D                D LII h

which gives, yb q ~ 3398'10 Deflect/on from pressure lshear, K~:=-0.3 2'In a I+ rp 2 I-2 rp In-b m'vg a 2 b a

tG" which gives, Ksa ~%.013 and ysq 3 715 10 hh Deflection from pressure//hub stretch,

                                                                                             -P force.L orce '=tt (a
                                       - b ) DP avg                            y stretch ttb.2E which gives,                   P force         2 176 l(P           and        y stretch    6 034 10 COMED PL Evaluation                                      Valve ID: 2ICS'MOV122                                                 page 2 PICS122A.MCD

Niagara Mohawk Power Corporation NMP 2 Page~i>~ Nuotear Engineering CatoLrlation Cont. Sheet A10.1-AD403, Rw. 01 Originatorloate

'Dao r~po JP r ~M </r 5 ~f7i                            ChN'kar/Ost Iggp Total Deflection due to pressure,                        yq  '     bq+ y sq+ y stretch which gives,            y   = -7.174 10 Addilional Geometry Factors ro.'=a L3 .=

ro

4a ro a 2

                               + I ln a

ro ro

                                       +  - I a

2 L9 .'= a

ro I+v 2 In + I-v a ro 4 I ro a 2 which gives, L3 =0 and L9 =0 P Deflection from seat load/bending, w'- ] ybw' D C2 rpC9 C8

b L9

                                               - foC3 +L3 b

which gives, y bw =-1.43

o Deflection from seat load/shear, Ksa:=-1.2 ln-a b y:= Ksa tG which gives, Ksa . 182 y ~ -1.174'10 Deflection from seat load/hub compression, L

                         -2'1t a   2 y compr                          which gives,                y~mpr =-I 002'10 ttb Total Deflection from unit seat load, y w:=y bw+y sway compr                      which gives,            yw       2621 10 Equilibrium contact load distribution, w equilibrium ' yq              which gives,             equilibrium Load per seat =         2 tt a yq    988.835 yw Pressure Locking Force, COMED PL Evaluation                            Valve ID: 2ICS'MOV122                                               page 3 PICS122A.MCD

Niagara Mohawk Power CorPoration NMP 2 Pagegl ot i >7 Nuctear Engineering Catculation Cont. Sheet

A10.1-AO403. Rev. 01 Originator/Date Checker/Date WC ms>c/ A ~ /g//25'lf7 Vq F pres Iock 2 +a (p cos(e) sin(e)) 2 which gives, F pres lock = 895.433 Yw Effect Force, au:=0 1'iston P F pistcn street 'D stem 2

                                            '(P hcnnet- Penn}            which give,        pistcn efreet =502655 "Reverse Piston Effect" Force, F vert.'= n a          2 P bonnet up    down
                                                             -

sin(e) which gives. F ~ 1.015'10 Total Force Re uired to Overcome Pressure Lockin F total:=F pres lock+ Fpo+ F vert- F piston effect which gives, F >< =1.113735 10 ACTUATOR CAPA8ILITYt Actuator Model/Size: = SMB-0-25 Motor Torque Output: TQm:= 25.0 ft- lbs Gear Ratio: OGR:= 43.69 Application Factor: Af:=0.9 Pullout Efficiency: Eff:=0.4 Reduced Voltage: RV:=0.806 Torque Output: TQout:= TQm RV OGR AfEff TQout = 316.927 ft- Ibs Stem Factor: Thrust Capability: THcap: = TQout Sf THcap Sf:= 0.019627 Is615 10 Ibs ENHANCED PRESSURE LOCNNG METHODOLOGY: KEI:=1.20 Thrust Mtutpn:= THcsp- (Fmmi KHI} Thrust Margin ~ 2.783 ~ 10 Ibs

== Conclusion:== Open Thrust Margin is positive, therefore this valve and actuator are likely to overcome the theoretical pressure locking conditions evaluated. COMED PL Evaluation Valve lD: 2lCS MOV122 page 4 PICS122A.MCD

Niagara Mohawk Power Corporation NMP 2 PagegZof/3 ~

Nuclear Engineering Calculation Cont. Sheet

Ato.t-AD403. Rev. 01 Originator/Date Checker/Date

      ~,~,       A'.          c./,];ZPP                                "r-i+7 Valve ID no: 2ICS MOV128 Re uired          0 enin Force Defernminafion under Pressure Lockin Conditions COMED Method DESIGN INPUTS:

Design Basis Conditions at time of Pressure Locking Event: Upstream pressure(psig), Pp.=1200 Valve Bonnet pressure(psig),Pbonnet '=1200 Downstream pressure (psig), P do .=0 Valve Disk Geometry: r hub radius, b:= 3.063 mean seatradius, a:=4.45 average disk thickness, t:=1.012 hub length, L:= 0.188 seat angle, a:= 10 0:=-a ft 2 180 8 0.087 Valve Disk Material Properties: 8 ishalfdiskangle u modulus of elasticity, E:=29400000 Poisson's Ratio, v:=0.3 Other Valve Parameters: Valve Stem Diameter, D ~.= 2.5 Static Unseating Thrust, F po 17995

                                                                         ¹ (reference: Test 10, 5f4N5)

Valve Factor VF:=0.6 (reference: NER-2M-010) CALCULATIONS: Coefficient of fnct/on between disk and seat, It: = cue) sin(6) It =0.631 (reference ¹6) up+ down Average DP Across Disk, DP avg .'=P bonnet gives, DP avg 600 2 Disk Sfiffnes Constants, D:= Et and G:= E l2(1-') 2 (1+v) which gives, D =2.79 10 and G =1.131 ~ 10 Geometry Factors, C2'.=-I 4 I - b

a I+2 In a b C3

                                                                           .'.=

b 4a, b

a I In a

b

b a I C8:=-I I+ 2

b C9 a

                                                                               '=-b I+v In 2

a b

I-v 4 I b a 2 which gives, C2 0.043 C 3 ~0.004 C8 08'6 C 9 ~0.23 COMED PL Evaluation Valve ID: 2ICS MOV128 page 1 PICS128A.MCD

Niagara Mohawk Power Corporation NMP 2 Page Zgofi S Nuclear Engineering Calculation Cont. Sheet Rev. 01 7'10.1-AD403, Origina! or/Date Checkor/Da! e 2 c/is Jap p- j-f7 Addit/onal Geomet/y Factors, rp '.=b 2 4 2 2 I+4 fp - fp -4. fp fp L 11 '= 5 ~ 2+ ln 64 a a a a rp L17.'=-I I - 4 I-Y - 4 I a 0 4

a 0 2 I+(I+Y) ln a rp which gives, L I I =3.398 10 and L17 ~0.04 ~ Moment Factors, DPavga C9 ( Mrb' 2ab 2

                                                       'pj             1(                  ~b:=

2b

                                                                                                       .'"'( *-     0*)

C8 which gives, M rb -<98.979 and Qb I 021 Ip k Deflection from pressure(bending, 4 3 avg a yb '=M*C2+Qb' a a C3- LII o o o which gives, yb q =-1.078-10 Deflection from pressure Ishear, 2 2 r'p K m'DP avg I+ rp a 21n - 21n-a K~:=-0.3 ~ I b a b t.G III which gives, K sa %.066 and y sq ~%.877 10 Deflection from pressure lhub stretch, P fpfee 't (a b ) DP avg y stretch '= P fpfce'L ttb 2E which gives, P fp~ =1.964 10 and y ~h =-2.131 10 COMED PL Evaluation Valve ID: 2ICS'MOV128 page 2 PICS128A.MCD

Niagara Mohawk Power Corporation NMP 2 Nuctear Engineering Calculation Cont. Sheet A10,1.AD403, Rev. 01 Originator/Date Checker/Date uo~r~~ <-d~ p c/~Vpp Total Deflection due to pressure, yq: ybq~ysq+y~~h which gives, y =-1.787 10 Additional Geometry Factors ro.'=a L3,- ro 4a ro a 2

                                +I    In  +

a ro ro

a 2 I L9 -'= a

ro I+v 2 In a ro

I-v I-4 ro a 21 ybw Ksa:=-

              '9  a3.w 1.2 D

which gives, Deflection from seat load/bending, ro ro

a C2 ro C9 C8 Deflection from seat load!shear, In-b b L3 =0 ro.c3 y ~.'=Ksa b w:= I

tG

                                                               + L3 and which gives,
                                                                                    'L9 which gives, 0

y bw =-3.67 Ksa W.448 10 y ~ ~-,1.743 10 Deflection from seat load/hub compression, L

                          - 2'tt'a   2 y compr
                      'tb                        which gives,               y compr    3'033 10 Total Deflection from unit seat load, y w:=y bw+y ~+y compr                           which gives,           y w =-5.443 10 Equilibrium contact load distnbut/on, w equiIibrium         yq           which givest          w cqtulibzum     328.415 yw Load per seat =            2 tt a yq  =9.183 ~ 10 yw Pressure Locking Force, COMED PL Evaluation                               Valve ID: 2ICS'MOV128                                           page 3 PICS128A.MCD

It Niagara Mohawk Power CorPoration NMP 2 Pagano/ /97 Nuctear Engineenng Catculation Cont. Sheet

A10.1.AD403, Rev. 01 Originator/Date Checker/Date Z c Xs ~ ~ v A. /P'/t,r Zzlpp ~re tr 'I" F pres lock 2 tt a (p Yq cos(1) - sin(e)) 2 which gives, F pres lock = 9.938'0 3 Vw Piston Effect Force, Pau '.=0 r tt Fpinon WmtDm '(Phoner Penn) which g/ves, F piston effec "Reverse Piston Effect" Force, Pttoten)]sin(S) which gives, F v~ 6 506 10 Frets.=[as (2Phonnet up Total Force Re uired to Overcome Pressure Lockin F total l= F pres lock+ F po+ F vert - F piston which gives, F >~ 2.854914.10 ACTUATOR CAPABILITY: Actuator Mode! ISize: = SB-2-60 Motor Torque Output: TQm .'=58.37 ft- 1bs Gear Ratio: OGR: = 72.01 Application Factor: Af:=0.9 Pullout Efficiency: Eff:=0.4 Reduced Voltage: RV: = 0.8703 Torque Output: TQout:= TQm RV OGR AfEff TQout = 1.146 10 ft- 1bs Stem Factor: Sf:= 0.029481 TQout Thrust Capability: THcap:= THcap ~3.888 10 1bs Sf NOTE: RV IS SQUARE IF ACTUATOR IS AC. ENHANCED PRESSURELOCIQNG METHODOLOGY: KEI:=1.20 Thrust Mtntpn:= THoap (F n,uu KE!) Thrust Margin 4.617'10 1bs

Conclusion:

Open Thrust Margin is positive, therefore this valve and actuator are likely to overcome the theoretical pressure locking conditions evaluated. COMED PL Evaluation Valve ID: 2ICS MOV128 page 4 PICS128A.MCD

Niagara Mohawk Power Corgoration NMP 2 Calculation Cont. Sheet Pageant/'0 7 Nuoiear Engineering A10.1-AD403, Rev. 01 cheekerioste~ r/</r7 Valve ID no: 2ICS'MOV129 Re uired 0 enin Force Deternmination under Pressure Lockin Conditions COMED Method DESIGN INPIJTS: Design Basis Conditions at time of Pressure Locking Event: Upstream pressure (psig), P .=76 Valve Bonnet pressure (psig), P bonn<< = 2799 p Downstream pressure (psig), P do~ 0 Valve Disk Geometry: hub radius, b:= 2.25 mean seat radius, a:= 3 average disk thickness, t:=0.378 hub length, L:=0.125 seat angle, u:=7 e:=-'" e =o.o61 2 180 Valve Disk Material Properties: e ishalfdiskangle a modulus of elasticitY, E:=29400000 Poisson's Ratio, v:=0.3 Other Valve Parameters: Valve Stem Diameter, D <~.= 1.5 Static Unseating Thrust, F~.=5924 (reference: Test 12, ¹ 6/QM3) Valve Factor VF:=0.65 (reference: NER-2M-010) CALCULATIONS: Coefficient of friction between disk and seat, It.,= cue) It 0.676 (reference ¹6)

                                                                      - sin(e)

Pup+Pdo~ Average DP Across Disk, avg 'onnet 2 gives; DP av< =2.761 ~ 10 Disk Stlffnes Constants, D:= Et and G:= E u (1 .*j 2 (1+v) which gives, GeometryFactors, D =1.454 C2.'=- 1 4 10 I - b

a and I+2.1n a, G =1.131 ~ 10 b C3'.= b 4a b

a a

                                                                                           +1 ln  +

b b a

                                                                                                               -   I C8.=-  1 2

1+ v+(1- v) b a 2 C a 1-9.--b I+v ln 2 a b

1 4 v b a 2 which gives, C2 0.028 C 3 ~0.002 C 8 ~0.847 C 9 ~0.198 COMED PL Evaluation Valve ID: 2ICS'MOV129 page 1 PICS129A.MCD

Niagara Mohawk Power CorPoration NMP 2 PageMot tp T Nuctear Engineering Catcutation Cont Sheet A10.1-AD403, Rw. 01 Onginator/Date Checker/Date Wc,~~a, A'.Quar S c./ip~ Additional Geomet/y Factors, rp .'=b 2 4 2 2 fp fp 11 I I+ 4 rp

                                      -5    rp
                                                    -4            ~

2+ ln-64 a a a a rp L 17 I

           '.=-.

4 I- - I v 4 I rO a 4

rO a 2 I +(I+ v) In a rp which gives, L I I =1.453 10 and L 17 =0.027

Moment Factors, Mg:=- DP avg cs a 2 C9 2ab., (

0 j-"I7 ~b:= 2b

                                                                                                  '"'('-      0')

which gives, Mrb =%03.057 and Qb ~2.416 10 Detiection from pressureIbend/ng, 4 3 avg.a yb '.=Mrb- C2+Qb a C3-a LII o o o which gives, yb q --8.049 10 Deflection from pressure Ishear, 2 2 K:=-0.3 2 In a I+ 'o I-21n- 'o sa'vg a sa' a b tG which gives, Ksa 041 'nd y sq ~-2.404 10 Deflection from pressure /hub stretch,

                                                                                        -P force L P fore'0    Tt (a       b ) DP avg                          y stretch '=

ttb 2E which gives, P force 3 415 10 and y stretch -4.565 10 COMED PL Evaluation Valve ID: 2ICS MOV129 page 2 PICS129A.MCD

Niagara Mohawk Power CorPoration NMP 2 Page gd Nuotear Engineering Calcutatton Cont. Sheet oflVV'10.1-ADOOS, Rev. 01 Ortginatorioate checker/Dmto~ p/j/rp Woe~-. 4.Cavy c/~/pp Total Deflection due to pressure, yq'=ybq+ysq+yst tch which gives y q =~001 Addilional Geometry'actors ro.'=a L3 = ro 4a ro a 2

                                +1     1n r

a ro

                                               +  -1 a

2 L9 .'. a

ro 1+v 2 ln a ro

1 v 4 1-ro a which gives, L3 =0 and L9 =0 Deflechon fram seat load/bending, w:= I

                                          -L9 -

IP

              '.=-

as.w C2 ro C9 roC3 yb +L3 which gives, y bw =-1.088 10 D C8 b b Deflection from seat load/shear, ro ro

Ksa: =-1.2 a In-b y~'.=Ksa-a tG which gives, Ksa <.345 y sw ~-2.423 10 Deflection from seat load/hub compression, L

                          -2 rta     2 y compr '=                           which gives,               y compr =-252'10 rtb 7otal Deflection from unit seat load, y w:=y bw+y sw+y compr                         which gives,            yw     1332 10 Equilibrium contact load distribution, yq            which gives,         w cqtttTtbrtttm 787.968 cqttitibrtttm w

Load per seat = 2 rt a yq = 1.485 10 yw Pressure Locking Force, COMED PL Evaluation Valve ID: 2ICS MOV129 page 3 PICS129A.MCD

lg Fy

Niagara Mohavttk Povtrer Corporation NMP 2 Page2 lot I 7 7 Nuclear Engineering Calculation Cont. Sheet A10.1.AD403, Rev. 01 Originatorloate 'Qp~r y>> <. Cecq /gQ j /F7 Checker/Date

                                                                              ,g HII Vq F

p 1 oc k 2 ta 1 1'w ( p co s ( 0 ) s in ( 8 ) ) 2 whi ch gi ve s, F p, 1 oc Piston Effect Force, P au:=0 "piston streettem'i2 I 1t bonnet atm) piston effect "Reverse Piston Effect" Force, F vett tt a 2 P bonnet P P tlown stn( ) which gives F vert 9 532 1 0 up Total Force Re ulred to Overcome Pressure Lockln F total: F pres 1ock+ F po t F >crt F pisto which gives, F <<~ =2.872746 10 ACTUATOR CAPABILITY: Actuator Model /Size: = SMB-00-10 Motor Torque Output: TQm:= 10.0 ft- lbs Gear Ratio: OGR:=36.2 Application Factor. Af:=0.9 Pullout Efficiency: Eff:=0.4 Reduced Voltage: RV: = 0.8252 Torque Output: TQout:= TQm RV OGR.Af Eff TQout 107.54 ft- Ibs Stem Factor. Thrust Capability: THcap '.= , TQout Sf Sf:= 0.015334 THcap =7.013 10 'bs ENHANCED PRESSURE LOCNNG METHODOLOGY: KEI:= 1.20 Tbrnst Margin: = THoap (F >>mt KEI) Thrust Margin ~ -2.746 10 1bs

Conclusion:

Open Thrust Margin ls negative, therefore this valve and actuator are unlikely to overcome the theoretical pressure locking conditions evaluated. COMED PL Evaluation Valve ID: 2ICS MOV129 page 4 PICS129A.MCD

0 Niagara Mohawk Power Corporation NMP 2 Page QO/ /P 7 Nuclear Engineering Calculation Cont. Sheet A10.1 AD403. Rev. 01 Originator/Date Checker/Date

                                         ~/i~/vr Valve ID no: 2RHS MOV115 Re uiredO enin                         ForceDeternminafionunderPressureiockin                                            Condifions COMED Method DESIGN Design Basis Conditions at time of Pressure Locking Event:
                                                .= 85            Valve Bonnet pressure (psig), P bonnet '= 7105 INPUTS'alve Upstream pressure (psig),                    P Downstream pressure (psig), P do~                           0 Disk Geometry:

hub radius, b:=5.75 mean seat radius, a:=7.703 average disk thickness, t;=1.644 hub length, L:=0.25 seat angle, a '= 10 0:=-'" 0 -0.087 2 180 Valve Disk Material Properties: 0 ishalfdiskangle a modulus of elasticity, E:=29400000 Poisson's Ratio, v:=0.3 Other VaNe Parameters: Valve Stem Diameter, D ~.= 2.375'tatic Unseating Thrust, F po 12604

                                                                                    ¹ (reference: Test 4, 6/24/93)

Valve Factor VF:= 0.5 (reference: NER-2M-010) 1 CALC ULATIONS: Coefficient of fnction between disk and seat, It:= ~<0) sin(0) It 0.521 (reference ¹6) P~+Pdo~ Average DP Across Disk, avg 'onnet 2 gives, DP ag =7.063 10 Disk St/ffnes Constants, Et 3 and G:= 12 I-v 2 (1+v) which gives, D =1.196 10 and G 1.131 ~ 10 Geometry Factors, C 2'.=-I 4 I - b

a

I + 2 In a

b

".

C 3 ',= b 4a b

                                                                                                    +I a

In a

b

b a

                                                                                                                             - I C8   I 2
                                               '+ v+(I - v)        b a

2 C9.-- I- In + 2 which gives, C 2 ~0.029 C 3 ~0.002 C 8 ~0.845 C9 =02 COMED PL Evaluation Valve ID: 2RHS MOV115 page 1 PRHS115A.MCD

0 Niagara Mohawk Power Corporation NMP 2 Pagea/of/'3T Nuclear Engineering Calculation Cont. Sheet A10.1-AD403, Rev. 01 Originator/Date Wc~i~~ W.imp c.gp/pp Chaclterllhte e

                                                                                     ~Q g/~

Additional Geometry Factors, rp"=b 2 4 2 2 L II '= I 1 +4 0 - 5 - 4 0 0 2+ rp ln- a 64 a a a a rp L17 I 4 I- I-I-v 4 a 0 4 rp a 2 I+(I+v) In- a rp which gives, L I I =1.535 10 and L17 ~0.028 Moment Factors, Mrb '.=- DPavga C8 2

                                ~  -

C9 / 2ab ~a rp,i - L17 2b

                                                                                                           '(     Oi which gives, Mrb =-1.57            10    and                   Qb     1.614 10 Deflection from pressureibending, 4
                           'rb'C2+Qb'C3 a

D . D a "avg'b D

                                                                                           'Lll which gives,                yb q =W.OOI Detiecfion from pressure /shear, K~:=-0.3 21n         a -

I+ rp 2

                                                        ~   1-21n-     rp                              stt'vg a2 b   -'

b t.G which gives, K aa =%.043 and y~ = %.605'O DefieÃon from pressure lhub stretch,

                                                                                               -P forciL Pforca't   (a      b ) DPavg                                     ystretch-ttb 2E which gives,               P  f0~         5.829 10                  and         y ~t h    -2.386 10 CQMED PL Evaluation                                Valve ID: 2RHS'MOV115                                                      page 2 PRHS115A.MCD

Niagara Mohawk Power Corporation NMP 2 Page32of r&7 Nuotear Engineering Calculation Cont. Sheet A10.1-AtM03, Rev. 01 Originatorloate Checker/DIt ~ p/1)gg Vo~rvp e 4.Qm a c /(s lp 7 Total Deflection due to pressure, yq: ybq+ysq+y~~h which gives,, y q =%.002 Additional Geometry Factors r "=a L3 ro 4a ro a 2

                             +I     In +  - I r

a ro a 2 L9.= a

rp I+v 2

In a rp

I- I-4 v ro a 2 which gives, L3 =0 and L9 =0 Detlection from seat load/bending, w:= I ybw'9 D C2 rpC9 C8 b

fpC3 b

                                                             + L3      which gives,         ybw =-2.338       10 Deflection from seat load/shear, Ksa: =-1.2    In-                   y sw  '=~'Ga              which gives,           Ksa     -0.351 a       b y'w      -1.454'10 Deflection from seat load/hub compression, L
                        -2'tt'a 2 y compr
                     'tb                       which gives,               y~     r =-1.981
                                                                                              ~

10 Total Deflection from unit seat load, y w:=y bw+y sw+y eompr which gives, yw 3'811 10 Equilibrium contact load distnbution, w equiiibritm:= yq which gives, w equilibrium 5'6N IP yw Load per seat ~ 2 tt a yq = 2.712 10 yw Pressure Locking Force, COMED PL Evaluation Valve ID: 2RHS'MOV115 page 3 PRHS115A.MCD

0 Niagara Mohawk Power Corporation NMP2 Page&of /3'7 Nuoiear Engineering Calculation Cont. Sheet A10.1-AD403, Rev. 01 Originatot/Date Checker/Date z~~g~g; A. 4 ~ 8/zHs7 lock'= 2 11 a " Yq (p'cos(e)- sin(e)) 2 " whichg/ves, F pres loci; pres Yw Piston Effect Force, piston etreot

                          '=    'tem '(    bonnet       atm)          whicl gives,      F piston egect "Reverse Piston Effect" Force,
                . I Pont/=[a       a  (2 P bonnet      np    Pttonn)] sin(g)             which gives,       F~ =2.295     10 Total Force Re uired to Overcome Pressure Lockin F totd:=F p~ I~k+Fpo+F v~- Fpi~n                  erect which gives,       F to  d     4.447654 10 ACTUATOR Actuator Model ISIze:                                                                     = SMB-0-25 Motor TorqueCAPABIUTY'Qout Output:                                                      TQm .'= 24.67           ft- lbs Gear Ratio:                                                                        OGR:=58.13 Application Factor:                                                                  Af:=0.9 Pullout Efficiency:                                                                  Eff:=0.4 Reduced Voltage:                                                                     RV:= 0.8767 Torque Output:                   TQout."= TQm RV -OGR        AfEff                TQout = 396.802          ft- lbs Stem Factoi:

Thrust Capability: THcap: = Sf THcap Sf: = 0.023664 1.677 10 lbs NOTE: RV IS SQUARE IF ACTUATOR IS AC. Jt ENHANCED PRESSURE LOCIQNG METHODOLOGY: KEI:= 1.20 Tbrnst Margin:= THoap (pmmt KBI) Thrust Margin ~ -5.17 10 1bs

Conclusion:

Open Thrust Margin Is negative, therefore this valve and actuator are unlikely to overcome the theoretical pressure locking conditions evaluated. COMED PL Evaluation Valve ID: 2RHS'MOV115 page 4 PRHS115A.MCD

Niagara Mohawk Power Corporation Nuotear Engineering NMP 2 Calcutation Cont. Sheet Pageggf 1 37 A10.1.AD403. Rev. 01 Originator/Date

                                           <</c'r/r 7 Ch<<kerlD le
                                                                                                >// ~

Valve IDno: 2RHS'MOV116 Re uiredO enin ForceDeternminationunderPressureLockin Conditions COMED Method DESIGN Design Basis Conditions at tIme of Pressure Locking Event: INPUTS'alve Upstream pressure (psig), P .= 133 Valve Bonnet pressure (psig), P bonnet = 1868 p Downstream pressure (psig), P down 0 Disk Geometry: hub radius, b:= 5.75 mean seat radius, a.'=7.703 average disk thickness, t:= 1.644 hub length, L:=0.25 seat angle, a.=10 0:=-a tt 2 180 0 =0.087 Valve Disk Material Properties: 0 ishalfdiskangle a modulus ofelasÃcity, E:=29400000 Poisson's Ratio, .=0.3 Other Valve Parameters: Valve Stem Diameter, D ~ ..=2.375 Static Unseating Thrust (reference: Test ¹ 10, F po 7/10195) 16894 Valve Factor VF:= 0.5 (reference: NER-2M-010) CALCULATIONS: cos(0) Coefficient of friction between disk end seat, it:=

VF I sin(0) p 0.521 (reference ¹6) up+ "down Average DP Across Disk, DP avg '.= P bonnet glvesr DP av I 802 10 2 Disk StNnes Constants, D;= and G:= i2. (1 ') 2 (1+v) which gives, D 1.196 10 and G =1.131 ~ 10 GeometiyFactors, C2.=-I 4 I- b

a 1+2 ln a b C3'.= b 4a b

a I ln a b

b a I C8:=-'+I 2 v+(I- v) b a 2 C a

9,--b I+v In 2 a b

I v 4 I b a 2 which gives, C2 0.029 C 3 =0.002 C8 0.845 C 9 =0.2 COMED PL Evaluation Valve ID: 2RHS'MOV116 page 1 PRHS116A.MCD

0 w}

Niagara Mohawk Power Corporation NMP 2 Page'PS of ~>> Nuctear Engineering Calculation Cont. Sheet Ato.t-AD403, Rev. 01 Originator/Date Checkerloate

+~~ape +-OW2 r Xp(gp                                                                      ~g~ /p Additional Geometry Factors,                                     rp .'=b 2               4               2                2 L  1 1
            '.= I 1  +4    -  -4 fP 5

rP rP

2+ In fP 64 a a a a rp L 17 -=-.I I I- v I - 4 rp a 4

                                                   -  rp a

2 I + (I 1- v) In a rp which gives, L 1,1 =1.535 10 and L17 =0.028 Moment Factors, 2 DPavga C9 / ~ (a -rp (-L17 'rib.- '"'. (a'- r,*j C8 2ab 2b which gives, 3 M~ =-4.005 10 and Qb =4 116 IO Defiedion from pressure/bending, 4 3 avg.a

                             '=Mrb           C2+ Qb C3-a                   a yb D                   D                  D LII which gives,                    yb q ~-2.937          10 Detiection from pressure/shear, 2                                                         2 K ~:=-0.3 2 In         a b
                                         - I+

rp a I-2 rp In-b ysq m Pavg a which gives, K ~ ~&.043 and y sq -245 10 DefieBion from pressure /hub stretch,

                      "
                                                                                             -P force L P f     '    (a       b ) DP g                       y stretch   '

nb 2E v which gives, P fo~ 1.487'10 and y stretch %.087'10 COMED PL Evaluation Valve ID: 2RHS'MOV116 page 2 PRHS116A.MCD

lI I,

Nktgara Mohawk Povrer Corporation NMP 2 Page/cot r> W Nuclear Engineering Calculation Cont. Sheet A10.1-AD403. Rev. 01 Ortginatorloate Checker/Date ~~~~y~ ~. 8~ al~s/j~ ~le/e~ Total Deflection due to pressure, yq:=ybq+ysq+yst t h which gives, yq 5 448 10 Additional Geometry Factors ro;=a L3 ro

4a ro a 2 e- I In + - I a ro ro a 2 L9 .'= a

ro I+v 2 In ~ I-v I-a ro 4 ro a 2 which gives, L3 =0 and L9 ~0 Deflection from seat load/bending, w:= I ybw

                -  as.w D

C2 ro C9 C8 b L9 roC3 b

                                                                   +L3 which gives,             y bw "2.338'10 Deflection from seat load/sheer, Ksa .'=-1.2 ro ro

a In-b y sw .'= Ksa tG which gives, Ksa ~ <.351 y sw ~-1.454'10 Deflection from seat load/hub compression, L

                           - 2'tt'a ycompr'=                ' 2           which gives,                y       ~-1.981 ~ 10 2

ttb E Total Deflection from unit seat load, y w:=y bw+y sw+y compr which gives, y w ~-3.81I 10 Equilibrium contact load distribution, w equilibrium '= yq which gives, w equilibrium ~ 1.429 10 yw Load per seat = 2 tt a yq 6.918 10 4 yw Pressure Locking Force, COMED PL Evaluation Valve ID: 2RHS'MOV116 page 3 PRHS116A.MCD

Niagara Mohawk Power Corporation NMP 2 >>geN<</3 7 Nuclear Engineering Calculation Cont. Sheet A10.1-AO403, Rev. 01 Originator/Date Checker/Date Qc,~/~aug tie g/Z)l57 pres lock

                      "'a'(>' Yq Yw
                                                     )      (  ))v 'res                           lock
                                                                                                                ~

4 Piston Effect Force, P ~,=0 effectDstem'i bonnet atm) which gives, F p,st,n effect = 8.275 piston 10'Reverse Piston Effect" Force, Frets.'=[s a (2 Fbonnet-Pp-Pgo~)] sin(g) whichgives, F ~=5.854 10 Total Force Re uired to Overcome Pressure Lockin F total ' F pres lock+ F pp + vert F - F piston effect which gives, F >~ =.1.26883 ~ 10 ACTUATOR CAPABILITY: Model /Size: 'ctuator = SMB-0-25 Motor Torque Output: TQm '= 24.67 ft- lbs Gear Ratio: OGR:= 58.13 Application Factor: Af:=0.9 Pullout Efficiency: Eff:=0.4 Reduced Voltage: RV: = 0.8731 Torque Output: TQout: = TQm RV OGR AfEff TQout ~ 393.55 ft- lbs 'Stem Factor. Thrust Capability: THcap: = TQout Sf Sf: = 0.023664 THcap ~ 1.663 ~ 10 lbs NOTE: RVIS SQUAREIF ACTUATORISAC. ENHANCED PRESSURE LOCNNG METHODOLOGY: KEI:= 1.20 Thrust Margin - THcap (F toM KEi) Thrust Margin ~-1.356'10 lbs

Conclusion:

Open Thrust Margin is negative, therefore this valve and actuator are unlikely to overcome the theoretical pressure locking conditions evaluated. COMED PL Evaluation Valve ID: 2RHS'MOV116 page 4 PRHS116A.MCD

0 Niagara Mohawk Power Corporation Nuctear Engineering NMP2 Calculation Cont. Sheet Paggtrtri /P 7 A10.1.AD403, Rev. 01 Originator/Date Checirer/Date Valve ID no: 2RHS MOV4A Re uired 0 enin Force Deternmination under Pressure Lockin Conditions COMED Method DESIGN INPUTS: Design BasIs Conditions at time of Pressure Locking Event: e Upstream pressure (psig), P =325 Valve Bonnet pressure (psig), P bo << = 9677 Downstream pressure (psig), P down 0 Valve Disk Geometry: r 4 hub radius, b:=2.25 mean seat radius, a:=3 average disk thickness, t:=0.378 hub length, L:= 0.125 seat angle, a:=7 e:=-' ' -o.o61 2 180 Valve Disk Materfal Properties: e ishalfdiskangle a modulus of elasticity, E:=29400000 Poisson's Ratio, v:=0.3 Other Valve Parameters: Valve Stem Diameter, D <~ '.= 1.5 Static Unseating Thrust F po 6341 (reference: Test ¹ 5, t/7/97) Valve Factor VF:=0.5 (reference: NER-2M-010) CALCULA77ONS: Coefficient of fiiction between disk and seat, lt:= cope) I VF

                                                                       -  sin(e)

It 0.515 (reference ¹6) up ~ down avg 'onnet Average DP Across Disk, gives, DP avg 9 515 10 2 E.t 3 Disk Stlffnes Constants, and G'= u (i .*j 2 (I+ v) which gives, D 1.454 10 and G 1.131 ~ 10 Geometry Factors, C2 I

                               '.=-,I 4

b a

I+2 In a b C 3 .'= 4a b b

a I In a b

b a I C8.=-I 2 b a C9 --b a

1+v In 2 a b

I v 4 I b a 2 which gives, C2 0.028 C 3 =0.002 C 8 =0.847 C 9 = 0.198 COMED PL Evaluation Valve ID: 2RHS'MOV4A page 1 PRHS4AA.MCD

lj Niagara Mohawk Power CorPoration NMP2 Page5&f ~>> Nuctear Engineering Calculation Cont. Sheet A10.1-AtM03, Rev. 01 Originator/Date Checker/Date Wo+.~~-4.Ce g ~/~g/.~ Additional Geometry'actors, rp '.=b 2 4 2 2 I fp fp

                                             -4          fp                rp In ,         a I+4                5                            2+             ~

64 a a a a rp L17 4 1 I - 1 v 4 I - rP a 4 rP a 2 I+(I+v) ln a rp which gives, L I I =1.453 10 and L17 =0.027 Moment Factors, DP avg a Mrb ' 2.a b a -rp -L17 <b:- 2b

                                                                                                      .'"'(*-"*j C8 which gives, Mrb =-3.112        10    and              Q b ~8.325 10 Deflection from pressureibending, 4
                              '=Mrb C2+Qb C3-                               avg a                a yb                                                             L11 o                 o                 o which gives,                  yb q =<.003 Deflection from pressure/shear, 2                                                     2 K:=-0.3 Sa'           2 In a

I+ rp I 21n- rp ysq'= sa'vg b b which gives, K sa =%.041 and '8.286 y sq 10 Deflection from pressure lhub stretch,

                                                                                        .
                                                                                            -Pto~'L P f0~      tt (a       b ) DPavg                           y stretch '=

ttb 2E which gives, P to~ =1.177 10 and y ~~ ~-1.573 10 COMED PL Evaluation Valve ID: 2RHS'MOV4A page 2 PRHS4AA.MCD

Ih I~

Niagara Mohawk Power Corporation NMP2 Pagegoof is T Nuclear Engineering Calculation Cont. Sheet A10.1-AD403, Rev. 01 Originatorloate Qomrap . g. @goy /gy/< Total Deflection due to pressure, yq:=ybq+ysq+yg etch which gives, y q =.004 Additional Geometry Factors r .'=a L3 '= ro 4a ro a 2

                               + I In ~  - I a

r'0 ro a 2 ro a

L9,'= I+v ln 2

                                                                                        + I-v a

ro 4 I ro a 2 which gives, L3 =0 and L9 =0 Deflection from seat load/bending, w:= I ybw

D C2 ro C9 C8 b L9 ro C3 b

                                                           + L3      which gives,        ybw =-1.088    10 Deflection from seat load/shear, Ksa:=-      1.2 ro ro

a In-b y ~:= Ksa tG which gives, Ksa <.345 y sw ~-2.423 10 Deflection from seat load/hub compression, L y compr 'b

                       .  -2na E

2 which gives, y compr 2 52 10 9 Total Deflection from unit seat load, y w:=y bw+y sway compr which gives, y w =-1.332 10 Equilibrium contact load distribution, w equii;brium.'= yq which gives w equilibriu =2.715 10 yw Load perseat= 2 na yq =5.118 10 yw Pressure Locldng Force, COMED PL Evaluation Valve ID: 2RHS MOV4A page 3 PRHS4AA.MCD

Niagara Mohawk Power CorPoration NMP2 Page 'flor>> 7 Nuclear Engineering Calculation Cont. Sheet Ato.t-AD403, Rev. 01 Checker/Date Originator/Date 'Dc,mrs3 8 ~> s/ S/l567 ~,e trr1 F pres look 2 a a Yq (1 cos(e) - sin(e)) 2

                                                                         ~    ~

which gives, F pros 1001

                                                                                                   = 4.635 ~ 10 4 W

Piston Effect Force, P a~'.=0 P Pinon W~t:=S D n~ (Phoner-Pet which give~, F piston

Frets "Reverse Piston Effect" Force, I

                .
                .'=[s e ~

(2 P honnet P dorm) j'etn(tt) which gives, F y~ 3 285 10 up Total Force Re uired to Overcome Pressure Lockin F total l = F pros look + F po + F yurt - F piston 0@00 which gives, F <<~ =6.843527 10 ACTUATOR CAPABILITY: Actuator Model ISize: = SB-OOS-15 Motor Torque Output: TQm:= 14.18 ft- lbs Gear Ratio: OGR:= 36.2 Application Factor: Af:=0.9 Pullout Efficiency: EQ':=0.45 Reduced Voltage: RV:"-0.8538 Torque Output: TQout:= TQm RV OGR.Af Eff TQout ~ 151.549 ft- lbs Stem Factor. Thrust Capability: THcap: = TQout Sf Sf:= 0.018919 THcap = 8.01 10 lbs NOTE: RV IS SQUARE IF ACTUATOR IS AC. ENHANCED PRESSURE LOCNNG METHODOLOGY: KEI:= 1.20 Thrust Meripn:= THoep (p n,~ KEI) Thrust Margin =-7.411 ~ 10 lbs

Conclusion:

Open Thrust Margin is negative, therefore this valve and actuator are unlikely to overcome the theoretical pressure locking conditions evaluated. COMED PL Evaluation Valve ID: 2RHS MOV4A page 4 PRHS4AA.MCD

fp 0

Niagara Mohawk Power Corporation Nuclear Engineering NMP2 Calculation Cont. Sheet Page/Zof /$ 7 A10.1-AD4ta, Rev. 01 Orlglnalor/Date ~z/v r>p ~ 8 ~ 4/2'3/Y7 Checker/Date

                                                                                ~z/z/rg Valve ID no: 2RHS MOV4B Re uired                   0 enin Force Deternmination under Pressure Lockin Conditions COMED Method DESIGN INPUTS'esign Basis Conditions at time of Pressure Locking Event:

Upstream pressure (psig), P .= 325 Valve Bonnet pressure (psig), P bo~<< = 9677 p Downstream pressure (psig), P do .=0 Valve Disk Geometry: r hub radius, b:= 2.25 mean seat radius, a:= 3 average disk thickness, t:=0.378 hub length, L:=0.125 seat angle, a '.=7 e:=-' ' =o.o61 2 180 Valve Disk Material Properties: e ishalfdisk angle a modulus of elasticity, E:=29400000 Poisson's Ratio, v:=0.3 Other Valve Parameters: Valve Stem Diameter, D st .= 1.5 Static Unseating Thrust, F po 7324

                                                                                  ¹ (reference: Test 5, 6/16/96)

Valve Factor VF:=0.5 (reference: NER-2M-010) . CALCULAnONS: cope> Coefficient of friction between disk and seat, it:=

                                                                            ~(e)

I VF p 0.515 (reference ¹6) up down Average DP Across Disk DP avg gives, DP av< = 9.515 10 2 Et3 Disk SfNnes Constants, D:= and G:= n.(i-') 2 (1+v) which gives, D 1.454 10 and G 1.131 ~ 10 GeometlyFactors, C2.'=-I 4 I- b

a I+2 1n a b C3'.= . b 4a b

                                                                                                    +I a

In a b

b a

                                                                                                                              -I c8:=-I 1+v+

2 a 2 C9 --b a I-1+v 2 In a

b

I v 4 b a 2 which gives, C2 0.028 C 3 =0.002 C 8 =0.847 C 9 =0.198 COMED PL Evaluation Valve ID: 2RHS MOV4B page 1 PRHS4BA.MCD

, )pf Niagara Mohawk Power Corgoration NMP2 Pager/3of/3 7 Nuctear Engineering Calculation Cont. Sheet A10.1-AD003, Rev. 01 N.<~ i er.abp Originator/Date Checker/Date

       -~p-Additional Geometry Factors,                                    rp '=b 2             4                2             2
                             -5  -4                                      '0

64 1

                     ]+4 a

0 a 0 a 0 2+ a ln-L]7 4 1

1- 1-U 1-4

a 0 4 a 0 2 I+(]+Y) ln rp a which gives, L ll =1.453 10 and L]7 0.027 Moment Factors, Mrb '=- DP avg a C8 2 C9 2ab a -rp -L]7 which gives, Mrb -3.112 10 and Qb =8.325 ]0 Deflection from pressureIbending, 4 3 avga

                             '.=Mrb C2+Qb' C3-a                  a yb                                                            L]1 o                  o                o which gives,                 yb q ~      0.003 Deflection from pressure /shear, K ~:=-0.3        2 ]n'   - ] +

a

rp 2

1 - 2 ]n- rp ysq'= m'vg a 2 a b which gives, K sa ~%.04] and y'-8.286 sq 10 Deflection from pressure Ihub stretch, P force'L P force tt (a b~) DP y stretch avg ttb 2E which gives, p force ] ] 77 ] p and y stretch -].573 ]p COMED PL Evaluation Valve ID: 2RHS'MOV4B page 2 PRHS4BA.MCD

1 Niagara Mohawk Power Corporation NMP2 Peg~ Af/j7 Nuclear Engineering Calculation Cont. Sheet A10.1-AD403. Rev. 01 Originator/Date Checker/Date

      . >oA.e~z Qzz/sy                                            ~rWrZ Total Deflection due to pressure,                           yq:=ybq~ysq+yst        etch which gives,           yq    0 004 Additional Geometry Factors                           =a ro L3 .=

ro

4a ro a 2

                              + I In    +  - I a

ro ro a 2 L9 - a

ro I+v I-v 2 In a ro

4 I ro a 2 which gives, L3 =0 and L9~0 Deflection from seat load/bending, w:= I ybw:- a w C2 rDC9 D C8 b L9 fpC3 b

                                                              +L3 whichgives,             y bw -1.088    10 Deflection from seat load/sheer, ro ro

Ksa:=-1.2 a In-b y:=Ksa- a tG which gives, Ksa ~ <.345 y~~-2.423 10 Deflection from seat load/hub compression, L

                         - 2'll'a 2 y compr
                      'tb                      which gives,               y compr Total Deflection from unit seat load, y w:=y bw+y sw+y compr                         which gives,           y  =-1.332 10 Equilibrium contact load distribution, equiiibn~: =     yq           which gives,            equilibrium yw LOad per Seat        a-    2 ft a yq    5.118 10 4

yw Pressure Locking Force, COMED PL Evaluation Valve ID: 2RHS'MOV4B page 3 PRHS4BA.MOD

1 Niagara Mohawk Powir Corporation NMP2 Pagett+of W7 'uclear Engineering Catculatlon Cont. Sheet A10.1-AD403, Rev. 01 Originator/Date '3cmr wag A'- ~ &/isls7 Checker/Date Fpr s lock '(l' Vq W

                                                   )      (  ))                   g          pfe  loctu
                                                                                                              ~

4 Piston Etect Force, P ~'.=0 F piston '= ttu'D 2/'(P which gives, etrtmt stem bonnet Perm)

   "Reverse Piston Effect" Force, Fyett.'=    rt a   2 P bonnet                gown     .sin(0)          which gives,      F y~   3 285 10 up 1

Total Force Re uired to Overcome Pressure Lockin F total: = F pres toed p F po + F yett - F piston effect r which gives, F <<~ =6.941827 10 ACTUATOR CAPABILITY: Actuator Model ISize: = SB-OOS-15 Motor Torque Output: TQm:= 14.18 ft- lbs Gear Ratio: OGR:= 36.2 Application Factor. Af:=0.9 Pullout Efficienc: Eff:=0.45 Reduced Voltage: RV:=0.8741 Torque Output: TQout:= TQm RV OGR AfEff TQout ~ 158.841 ft- 1bs Stem Factor. Sf: = 0.018919 TQout Thrust Cap'ability: THcap:= THcap ~ 8.396'10 Ibs Sf NOTE: RV IS SQUAREIF ACTUATORIS AC. ENHANCED PRESSURE LOCNNG METHODOLOGY: KEI:= 1.20 Thrust Margin:= THcsp (F mmt KEt) Thtust Margin = -7.491 ~ 10 1bs

Conclusion:

Open Thrust Marginis negative, therefore this valve and actuator are unlikely to overcome the theoretical pressure locking conditions evaluated. COMED PL Evaluation Valve ID: 2RHS MOV4B page 4 PRHS4BA.MCD

U Niagara Mohawk Power Corporation NMP2 Pagefrcpf/3 7 Nuclear Fngineering Calcuhtion Cont. Sheet A10.1-AD403, Rev. 01 Checker/Date

         .~. ZA Originator/Date c/zylsp Valve ID no: 2RHS'MOV4C Re uiredO enin                          ForceDeternminationunderPressureiockin                                                  Conditions COMED Method DESIGN Design Basis Conditions at time of Pressure Locking Event:

INPUTS'alve Upstream pressure (psig), P 325 Valve Bonnet pressure (psig), P bonn<< = 9677 np Downstream pressure (psig), P down 0 Disk Geometry: hub radius, b:= 2.25 mean seat radius, a:= 3 average disk thickness, t:=0.378 hub length, L:=0.125 seat angle, a '.=7 e:=-' ' -0.06I 2 180 Valve Disk Material Propertie: 6 ishalfdisk angle a modulus of elasticity, E:=29400000 Poisson's Ratio, v:=0.3 Other Valve Parameters: Valve Stem Diameter, D st~ 1.5 > Static Unseating Thrust, F po 3798

                                                                                      ¹ (reference: Test 21, Tlt8/g5)

Valve Factor VF '=0.5 (reference: NER-2M-010) CALCULATIONS: coge) Coeftic/ent of frict/on between disk and seat, lt.=

                                                                                                                                          ¹6)

I VF sin(6) It = 0.515 (reference up ~ down gives,'P <<g = 9.515 Average DP Across Disk, <<g'bonnet ~ 10 Disk SNfnes Constants, Et:=

                                                                       'nd             G:=       E u(i-')                                     2.(1 + v) which gives,                D =1.454     10               and          G ~ I.I31 ~ 10 Geomet/y Factors,                   C2  .'=-I I -

4 b a I + 2 In a b

C 3 '.= +I b 4.a b a h b a

                                                                                                                           +  -I b

a C8.=-I 1+ v+(I- v) 2 b a 2 C a

9'.=-b 1+v In 2 a b

1-v 4 I b a 2 which gives, C 2 =0.028 C 3 ~0.002 C 8 =0.847 C 9 =0.198 COMED PL Evaluation Valve ID: 2RHS'MOV4C page 1 PRHS4CA.MCD

Niagara Mohawk Power Corporation NMP2 Pagegkfl~ 7 f Nuclear ngineering Calculation Cont. Sheet A10.1-AD403, Relr. 01 Checker/Date Originator/Date Ww~ g~ N. 8~ WiP/P'P r/ r7 Additional Geometry Factors, rp '.=b 2 4 2 2 fp fp fp fp I+ 4 -5 -4 In

LII = 2+ ~ 64 a a a a rp L17 .-- I-4 I I-Y I-4 a 0 4 a 0 2

I+(I+Y) In- a rp which gives, L I I =1.453 10 and L17 =0.027 Moment Factors, 2 Dpavga C9 I 2- f (a 0 ) 2h - L I7 avg 2 2 C8 2ab 2b which gives, Mrb -3.112 10 and Qb 8.325 10 Deflection from pressureIbending, 4 3 avg a yb .'=Mrb C2+Qb C3-a a D D D LII which gives, yb q ~%.003 Deflection from pressure Ishear, 2 2 K sa DP 'avg I+ I-21n-a

                                          -          rp                      rp                                  a K~'=-0.3 21n                                    ~

ysq'= b a b which gives, K sa ~%.041 and y sq =-8.286 10 DefleiWon from pressure Ihub stretch, P force'L P force tt'(a b j DP avg ystrctch-ttb 2E which gives, P fo~- 1.177 10'nd y ~etch = 1573'10 COMED PL Evaluation Valve ID: 2RHS MOV4C page 2 PRHS4CA.MCD

>E

g

Niagara Mohawk Power Corporation NMP2 Psge4<ot / 3 > Nuclear Engineering Calculation Cont. Sheet A10.1.AD403, Rev. 01 Onginatorloate Checker/Date w t"~ Qgp$ p Total Deflection due to pressure, yq'bq+ysq+ystretch which gives, y q =%.004 Additional Geometry Factors ro.'=a L3 '= ro 4a ro a 2

                                +I   In  +  - I a

ro ro a 2 L9 '.= ro a I-2 ln ro

4 r a

which gives, L3 0 and Deflection from seat load/bending, w:= I ybw.- asw C2 ro'Cg D C8 b L9

                                                 - ro'C 3 + L3 b

which gives, y bw -1.088'10 Deflection from seat load/sheer, ro ro Ksa: =- 1.2 In-b y sw:= KsR a which gives, Ksa = %.345 a tG y sw =-2.423 10 Deflection from seat load/hub compression, L

                      ,   -2tta '   2 which gives,                              ~

9 compr 2 y compr tt b Total Deflection from unit seat load, y w:=y bw+y sw+y compr which gives, y w =-1.332 10 Equilibnum contact load distribution, w equilibrium 'yq which gives, wequilibrium =2.715 10 yw Load per seat = 2 tt a yq yw 5.118 10 4 Pressure LocMng Force, COMED PL Evaluation Valve ID: 2RHS'MOV4C page 3 PRHS4CA.MCD

Niagara Mohawk Power Corporation Nuclear Engineering NMP2 Calculation Cont. Sheet Page+of/ + f A10.1-AtM03. Rev. Ot Checker/Date

                                         /PD $ lp7 F pres ]ock . = 2 tt a            (

Yq lt cos( t)) sin( 0) ) 2

                                                                                     ~      ~

which gives, F pres ]oc]

                                                                                                                 = 4.63 5- ~ ] 0 4 Yw Piston Effect Force,                                      Pat:=0 piston eg'act'=              'tem '(      honnet        aun)
                                                                                   "'o" tg"          piston street "Reverse Piston Effect" Force, Poets
                's'a 2'(g'Phennet
                . I Pup       Pttosan)j'stn(g)            which gives,       F ycrt   3 285 10 Total Force Re uired to Overcome Pressure Lockin F tpta]: = F pres ]ock+ F pp+ F ycrt               - F piston    cffcct which gives,          F <<~ =6.589227           10 ACTUATOR Model ISIze:

CAPABILITY'ctuator

                                                                                                    = SB-OOS.15 Motor Torque Output:                                                                          TQm: = 14.18            ft- 1bs Gear Ratio:                                                                                   OGR:= 36.2 Application Factor:                                                                            Af:=0.9 Pullout Efficiency:                                                                            Eff:= 0.45 Reduced Voltage:                                                                               RV: = 0.8727 Torque Output:                         TQout:= TQm RV OGR.Af Eff                             TQout ~ 158.332          ft- lbs Stem Factor:

Thrust Capability: THcap: =TQout Sf , Sf:= 0.018919 THcap 8.369 ~ ]0 Ibs . NOTE: RV IS SQUARE IF ACTUATOR IS AC. ENHANCED PRESSURE LOCNNG METHODOLOGY: KE]:= 1.20 Thrust Margin:= THcap (F>og KE1) Thrust Margin =-7.07'10 1bs

Conclusion:

Open Thrust Margin ls negative, therefore this valve and actuator are unlikely to overcome the theoretical pressure locking under conditions evaluated. COMED PL Evaluation Valve ID: 2RHS'MOV4C page 4 PRHS4CA.MCD

Niagara Mohawk Prrrrer CorPoration NMP2 Page jabot/Q7 Nuclear Engineering Calculation Cont. Sheet A10.1-AD403, Rev. 01 Originatorloate ga w~' $ r/a3/6 Valve ID no: 2SWP MOV17A Re uired 0 enin Force Deternmination under Pressure Lockin Conditions COMED Method DESIGN INPUTS: Design Basis Conditions at time of Pressure Locking Event: Upstream pressure (psig), P>> .= 123 Valve Bonnet pressure (psig), P bonn<< = 86 Downstream pressure (psig), P down 0 Valve Disk Geometry: hub radius, b:=4.94 mean seat radius, a:=5.75 average disk thickness, t:=0.789 hub length, L:=0.125 seat angle, a,'=7 0:=-a tt 2 180 0-0.061 Valve Disk Material Properties: 0 ishalfdisk angle a modulus of elasticity, E:=29400000 Poisson's Ratio, v.--0.3 Other Valve Parameters: Valve Stem Diameter, D ~.=2 Static Unseating Thrust, F po 6219

                                                                        ¹ (reference: Test 25, 3ttM5)

Valve Factor VF:=0.6 (reference: NER-2M-010) CALCULATIONS: cos(0) Coefficient of fnction between disk and seat, tt:=

                                                                 -     sin(0) tt =0.622    (reference   ¹6) up+     down Average DP Across Disk,               DP avg .'=Pbonnet                             gives,     DP av     24 5 2

Disk Stifl'nes Constants, Et 3 and G = E u (i - ') 2 (1+ v) which gives, D 1.322 10 and G 1.131 ~ 10 GeometryFactors, C2.'= 1+2 ln C3.'= +1 1n + -1 C8 .- 1 2 1+ v+ (1 v) b a C a

9.--b I+v ln 2 a b

1-v 1-4 b a 2 which gives, C2 0.009 C3 =4.316'10 C 8 ~0.908 C 9 ~0.124 COMED PL Evaluation Valve ID: 2SWP'MOV17A page 1 PSWP17AA.MCD

. ~ Niagara Mohawk Power Corporation NMP2 Page5lofr3 ar Nuctear Engineering Calculation Cont. Sheet A10.1-AD403. Rev. 01 Originator/Date Checker/Date Woevppw 4 Cw p cfg3/9) z/z/H7 Additional Geometry Factors, rp '.=b 2 4 2 2 ll '4 I I+4 fp 5 4 fp fp 2+ rp In- a a a a a rp L17 '=-.I 4 I I-I-U 4 a 0 4

a 0 2

I+ (I + Y) In a rp which gives, L 11 = 1.545'10 and L17 =0.009 Moment Factors, Mg:=- DP avg a C8 2

                                ~  -rp C9 2ab a               -L17 2b avg which gives, Mrb -8.73                  end            Qb =21.472 Deflection from pressure%ending, 4

avg a

                           '.=Mrb C2+Qb C3 a                  a yb                                                          .LII D                  O                  D which gives,              yb q ~-1.041 ~ 10 Deflection from pressure/sheer, K ~:=-0.3     2 In a

I+ rp 2

I-2 rp In-b ysq '= I'vg a 2 b a which gives, K sa %.013 and y'sq =-1.138 10 Deflection from pressure/hub stretch, P force'L Pra~.--a (a b ) DPaa< y stretch '= ttb 2E which gives, P fp~ 666.467 and y ~~ -1.848 10 COMED PL Evaluation Valve ID: 2SWP MOV17A page 2 PSWP17AA.MCD

II Niagara Mohawk Power Corporation NMP2 Page5'Zof r%T Nuclear Engineering Calculation Cont. Sheet A10.1-AtM03, Rev. Ot Originator/Date Checker/Date Z ~ ~p S. e~~/i slsp ~/zr~ Total Deflection due to pressure, yq'bq+ysq+ystretch which gives, yq 2 197 10 Additional Geometry Factors ro.'=a L3 '.= ro 4a ro a 2

                              + I In   +  - I ro a      ro a

2 L9 - a

ro I+v 2 ln + I-v I-a ro 4 ro a 2 which gives, L3 =0 and L9 =0 Deflection from seat load/bending, w:= I ybw -

              '=- a w C2 D C8 ro'C9 b

L9 fo'C3 b

                                                              + L3      which gives,       yb      I 437'10 "7

Deflection from seat load shear, l ro ro Ksa:=- 1.2 a ln- b y ~:=Ksa-tG a which gives, Ksa ~ %.182 y =-1.174 10 Deflection from seat load!hub compression, L

                          -2'lr a 2 y'compf    'ib                     which gives,                y compr Total Deflection f/om unit seat load, y w:=y bw+y sw+y compr                        which gives,            yw~ 2621'10 Equilibnum contact load distribution, yq w equilibrium
                              'w             which gives,              equilibrium Load per seat ~          2 tt a yq     302.831 yw Pressure Locking Force, COMED PL Evaluation                             Valve ID: 2SWP MOV17A                                           page 3 PSWP17AA.MCD

Niagara Mohawk Power Corporation NMP2 Calculation Cont. Sheet Page5$ of /37 Nuclear Engineering ~ s A10.1-ADO03, Rey. 01 Qflglnatof/Date Checker/Date

       ,. A. ~in/~ff/P 7                                               gtg rstg+

F pres look 2 s a Yq (p cos(8) - sin(8)) 2 which gives, F pres look 338 833

                                 /w Piston Effect Force,                             P au:=0 "piston cffect   '

stem 2

                                         '(  bonnet      atm)
                                                                          " "tp"     'iston       effect "Reverse Piston Eh'ect" Force, F v~',=     rt a  2 P bonnet               down       sin(8)          which gives,     F ert = 310.711 up Total Force Re uired to Overcome Pressure Lockin s

F total:=F pres look+ F po + F vert F ptston effec which gives, F >ud ~6.598367 10 ACTUATOR CAPABILITY: Actuator Model /Size: = SMB-0-25 Motor Torque Output: TQm:= 23.52 tt- lbs Gear Ratio: OGR;= 39.11 Application Factor: Af:=0.9 Pullout Efficiency: Eff:=0.4 Reduced Voltage: RV: = 0.8785 Torque Output: TQout:= TQm RV OGR AfEff TQout = 255.571 ft- lbs 'tem Factor: TQout Sf:= 0.019627 Thrust Capability: IHcap:= THcap ~ 1.302'10 1bs Sf NOTE: RV IS SQUARE IF ACTUATOR IS AC. ENHANCED PRESSURE LOCNNG METHODOLOGY: KEI:= 1.20 Thrust Margin:= THcap (F mmt KEI) Thrust Margin = 5.103'10 1bs

Conclusion:

Open Thrust Margin ls positive, therefore this valve and actuator are likely to overcome the theoretical pressure locking conditions evaluated. COMED PL Evaluation Valve ID: 2SWP'MOV17A page 4 PSWP17AA.MCD

0 Niagara Mohawk Povver Corporation Nuclear Engineertng NMP2 Calculation Cont. Sheet Page'574 / 97 A10.1 AD403. Rev. 01 Checker/Date 7/Z/gp Valve ID no: 2SWPMOV17B I Re uired 0 enin Force Deternmination under Pressure Lockin Conditions COMED Method DESIGN INPUTS: Design Basis Conditions at time of Pressure Locking Event: Upstream pressure (psig), P := 123 Valve Bonnet pressure (psig), P bonnet '= 86 Downstream pressure (psig), P doggy 0 Valve Disk Geometry: r hub radius, b:=4.94 mean seat radius, a '.=5.75 average disk thickness, t:=0.789 hub length, L:=0.125 seat angle, a:=7 e:=-'" e =o.o61 2 180. Valve Disk Materfal Properties: e ishalfdiskangle u modulus of elasticity, E:=29400000 Poisson's Ratio, v:=0.3 Other Valve Parameters: Valve Stem Diameter, " D <<~.= 2 Static Unseating Thrust F po 5862 (reference: Test 6, 8/2M4) ¹ Valve Factor VF:=0.6 (reference: NER-2M-010) CALCULATIONS: cos(e) CoeNicient of friction between disk and seat, p .'=

VF I sin(e) It 0.622 (reference ¹6) P down Pup + Average DP Across Disk, avg 'onnet 2 gives, DP av< 24.5 3 Disk SNfnes Constants, D:= and G:= i2. (1 ') 2 (1+v) which gives, D 1.322 10 and G =1.131 ~ 10 Geometry Factors, C2'.=-I 4 I - b

a

1+2.ln a b C3.=. b 4a b

a I In a

b

b a I C8.--I I+ v+(I - v) 2 b a C9 -- - In + I which gives, C2 0.009 C3 =4.316'10 C 8 >0.908 C 9 = 0.124 COMED PL Evaluation Valve ID: 2SWP MOV17B page 1 PSWP17BA.MCD

e Niagara Mohawk Power Corporation NMP2 Nuclear Engineering Calculation Cont. Sheet A10.1 AD403, Rev. 01 Originator/Date Checker/Date W~ ~c rP-Q~ ~gybe ~7/i/F7 Additional Geometry Factors, rp =b 2 4 2 2 I I+4 5 0 0 4 0 2+ rp In- a 64 a a a a rp L17 I 4 I-I-U 4 I a 0 4 a 0 2 I+ (I+ Y) In a rp which gives, L I I =1.545 10 and L17 =0.009 Moment Factors, avg'a C8 2 9 2ab p

                                          /2 -rp                                ~b=

DP avg 2b (

Oj which gives, M rb -8.73 and Qb 21.472 Deflection from pressure/bending, a2 a3 DP avg'a yb '.=Mrb C2+Qb' D C3- D LII D which gives, yb -1.041 10 Deflection from pressure /shear, 2 rp m.D avg .2 a K~:=-0.3 a 21n I+ I-21n-b rp ysq:= tG b a J which gives, K sa ~%.013 and y' -1.138'10 sq 0 Deflection from pressure/hub stretch,

                                                                                     -P forca.L

='(a'- b') DP,, y stretch .

ttb 2E which gives, P f0~0 =666.467 and y search 848 10 COMED PL Evaluation Valve ID: 2SWP'MOV17B page 2 PSWP17BA.MCD

'C Niagara Mohawk Power Corgoration NMP2 Page5cof/9 9 Nuciear Engineering Calcuhrtion Con!. Sheet A10.1-AD403, Rev. 01 OriginatorlOate W~~ ~ > 4. C'mg +~sky Total Deflection due to pressure, y q:=ybq<<ysq+ y stretch which givesr yq 2 197 10 AddNonal Geometry Factors '.=a r L3 - . ro 4a ro a 2

                                + I In   +

a ro r0 a 2

                                                        -I            L9    =

a I-ro I+v a 2 In + ro I v 4 r0 a 2 which gives, L3 =0 and L9 ~0 ~ Deflection from seat load/bending, w:= I

ybw ',=

              . a  w C2 D C8 roC9 b

L9' rpC3 b

                                                               + L3     which gives,         yb        I 437'10 Deflection from seat         loadl shear, ro ro Ksa:=-1.2         In-                y ~:=Ksa' a

which gives, Ksa =-0.182 a b tG y sw =-1.174'10 Deflection from seat load/hub compression, L

                          -2'tt a    2 y compr
                       '.b                      which gives,               y     p
                                                                                      -1.002'10 Total Deflectio from unit seat load, y w:=y bw+y sw+y compr                         which gives,            yw     2 621'10 Equilibrium contact load distribution, equilibrium   'hich yq yw gives,           equilibrium Load per seat =           2 tt a yq  =302.831 yw Pressure Locking Force, COMED PL Evaluation                             Valve ID: 2SWP MOV17B                                               page 3 PSWP17BA.MCD

e Niagara Mohawk Power Co/Poration NMP2 Page&ot/ 7 7 Nuclear Engineering Calculation Cont. Sheet

A10.1-AD403. Rev. 01 Originator/Date Thorn.ep-. At + /Flzglpp Checker/Date rs-rrÃ7 F pres loclt 2 a a Vq (p cos(0) - sin(0)) 2 which gives, F pres loci' 338.833

                                /w Piston Effect Force,                            P  at:=0 piston street
                         '= O'tem '< bonnet          p atm)          which gives,     F iston effect   270.177 "Reverse Piston Effect" Force, F vert      "'a P bonnet      P up P down                      which gives,     F ~ = 310.711 Total Force Re uired to Overcome Pressure Lockin F total: = F pres tock+ F po+ F 1/ert F piston effect which gives,         F <<< =6.241367          10 ACTUATOR CAPABlLITYt Actuator Model /Size:                                                                    = SMB-0-25 Motor Torque Output:                                                              TQm:= 23.52            tt-'bs Gear Ratio:                                                                       OGR:= 39.11 Application Factor:                                                                 Af:=0.9 Pullout Efficiency:                                                                 Eff:-"0.4 Reduced Voltage:                                                                    RV:= 0.8834 Torque Output:                TQout:= TQm RV OGR.Af Eff                          TQout = 258.43         tt- lbs Stem Factor.                                                                        Sf:=0.019627 TQout Thrust Capability:              THcap  '.=

Sf THcap = 1.317'10 lbs NOTE: RV lS SQUARE/F ACTUATORlS AC. ENHANCED PRESSURE LOCNNG METHODOLOGY: KEI:= 1.20 Thrust Margin: = THeap (F tong KBI) Thust Margin ~ 5.677 10 1bs

Conclusion:

Open Thrust Margin ls positive, therefore this valve and actuator are likely to overcome the theoretical pressure locklngconditions evaluated. COMED PL Evaluation Valve ID: 2SWP'MOV17B page 4 PSWP17BA.MCD

Niagara Mohawk Power Corporation NMP2 Page5$ br /%T Nuciear Engineering Calcutation Cont. Sheet At0,1-AD403. Rev. Ot Originator/Oate Checkedoate

'uow pro        /I Q 0 (p3/v
                    ~
                                                                   ~e/z/r7 ValvelDno: 2SWPMOV18A Re uired         0 enin        Force Defernmination under Pressure Lockin Conditions COMED Method DESIGN INPUTS:

Design Basis Conditions at time of Pressure Locking Event: Upstream pressure (psig), Pp.--108 Valve Bonnet pressure (psig), P bonnet =125 Downstream pressure (psig), P do~.=0 Valve Disk Geometry: hub radius, b:=4.94 mean sestrsdius, a:=5.75 average diskthickness, t:=0.789 hub length, L:= 0.125 seat angle, a .'=7 0:=- 2 180 0 =0.061 Valve'isk Matertal Properties: 0 ishstfdisksngle a modulus of elasticity, E:=29400000 Poisson's Ratio, v:=0.3 Other Valve Parameters: Valve Stem Diameter, D at~.--2 Static Unseating Thrust F po 8635

                                                                     ¹ (reference: Test 8, 3/17>95)

Valve Factor VF:= 0.6 (reference: NER-2M-010) CALCULATIONS: Coefticient of fnction between disk and seat, ~<0)

I VF sm(0) it =0.622 (reference ¹6) up+ down Average DP Across Disk, DP avg '= P bonnet" gives, DP av< ~71 2 Disk Sfiffnes Constants, Et and G:= E iz(i-v') 2 (I+ v) which gives, D ~1.322 10 and G ~1.131 ~ 10 GeometryFsctors, C2.'=- I- I+21n C3.= +I In 2 C8 '=-I 2 I+ v+ ( I - v) b a C9 --b a

I+v In 2 b a

I-v - 4 I b a which gives, C2 0.009 C3 ~4.316 10 C 8 =0.908 C 9 = 0.124 COMED PL Evaluation Valve ID: 2SWP'MOV18A page 1 PSWP18AA.MCD

Peg<~ref/V Niagara Mohawk Power Corporation NMP2 7 Nuclear Engineering Calculation Cont. Sheet A10.1&D003, Rw. 01 Orit/lnatorloate Checker/Date Wc ~~p t, N. des y cP~/pg r/s/f7 Additional Geomehy Factors, rp.'=b 2 4 2 2 L11 .'= 1+4. fp - rp 5 4 rp 2+ rp ~ In 64 a a a a rp L17.=- 4 I- I-4 ro a 4

rp

a 2

                                                               . 1~(1+v)       In rp a

which gives, L I I =1.545 10 and L17 ~0.009 Moment Factors, Mg:=- DPavga CS which gives, 2 C9 2ab (a -ro )-L lq o:= -") DP avg 2b ( Mrb =-25.298 and Q b ~62.225 Deflection fiom pressure/bending, DP avg a a2 yb '=Mrb C2+Qb D C3-a3 D LII D which gives, y bq 3.016.10 Deflection fiom pressure/shear, 2 2 rp K~:=-0.3 21n a I+ rp ~ 1-21n-b avg'o b a which gives, K sa =%.013 and y'-3.297'10 sq t Deflection from pressure /hub stretch, P force L P f .'= ll (a - b ) DP vg y stretch ttb 2E and y ~<h -5.355 10 which gives, P f0~ ~1.931 10 COMED PL Evaluation PSWP18AA.MCD Valve ID: 2SWP MOV18A'age 2

Niagara Mohawk Power Corporation NMP2 Pag~W 7 Nuclear Engineering Calculation Cont. Sheet A10.1-AD403, Rev. Ot CSginatorlDate Checkerloate Q~~ apy 4e @AD k- /g3/py r/rr'6 Total Deflection due to pressure, yq ' bq+ y sq+ y stretch which gives, yq H.367 10 Additional Geometry Factors ro:=a L3 - ro 4a ro a 2

                              + I In  +

a ro ro a 2 I L9 a

ro I+v 2 In a ro

I-v 4 I ro a 2 which gives, L3 0 and L9 =0, Deflection from seat loadlbending, w.'= I ybw'- asw C2 roC9 D C8 b L9 roC3 b

                                                            +L3 which gives,             yb     -I 437'10 Deflection from seat load shear, l ro      ro
                   ' In-b a

Ksa '.=- 1.2 y ~:=Ksa'G which gives, Ksa ~-0.182 y <-I;174 10 Deflection from seat load/hub compression, L 2'll'a 2 y compr' which gives, y compr ttb E Total Deflection from unit seat load, y w:=y bw+y sw+y compr which gives, y w =-2.621 ~ 10 Equilibrium contact load distnbution, w eqtniib.tm,.= yq which gives, w eqttitibritm = 24.291 w Load per seat - "2 tt a yq 877.591 yw Pressure Locking Force,, COMED PL Evaluation Valve ID 2SWP MOV18A page 3 PSWP'I 8AA.MCD

Niagara Mohawk Power Corporation NMP2 Paged/of /7 Nuclear Engineering Calculation Cont. Sheet A10.1-AtHSS, Rev. 01 Orig inatorloate Checker/Date m--;-A +lsPg/~p /is r<<. F pres iocle: = 2 rt a " Yq ( tt cos( 0) - sin( 6) ) 2 which gives, F pres loci = 98 1 . 925 W Piston Effect Force, Pat:=0 ft which gives, F piston effect "piston street,a'D stem '(phonnet peon)

 "Reverse Piston Effect" Force, F vert'.= ft a ~

2 P bonnet up

                                            - P do1tfn     sin(e)          whichgives,               Fy~     900428 Total Force Re uired to Overcome Pressure Lockin total 'res     lock+ po+         vert     piston effect whichgives,          F<<~         1.012465 10
                                                                              'CTUATOR CAPABILITY:

Actuator Model/SIze: = SMB-0-25 Motor Torque Output: TQm .'= 23.21 ft- lbs Gear Ratio: OGR:= 39.11 Application Factor. Af:=0.9 Pullout ENciency: Eff:= 0.4 Reduced Voltage: RV '-= 0.8789 Torque Output: TQout:= TQm RV OGR AfEff TQout = 252.432 ft- lbs Stem Factor. , Sf:=0.019627 Thrust Capability:, THcap .'=T out Sf THcap =1 286 10 lbs NOTE: RV IS SQUARE IF ACTUATOR IS AC. ENHANCED PRESSURE LOCNNG METHODOLOGY: KEI:= 1.20 Thrust Margin:= THoap (F to% KEI) Thrust Margin 711.881 Ibs sl

Conclusion:

Open Thrust Margin ls positive, therefore this valve and actuator are likely to overcome the theoretical pressure locking conditions evaluated. COMED Pl. Evaluation Valve ID: 2SWP'MOV18A page 4 PSWP18AA.MCD

Niagara Mohawk Power Corporatton NMP2 Pape scut I PT Nuclear Engineertng Calculation Cont. Sheet A10.1-AD403, Rev. 01 Originato/Date

          ,-.w. e; -E~/~

Checker/Date gled f >/i/~7 Valve ID no: 2SWP'MOV18B Re uired 0 enin Force Deternmination under Pressure Lockin Conditions COMED Method DESIGN INPUTS: Design Basis Conditions at time of Pressure Locking Event: Upstream pressure (psig), P p,=108 Valve Bonnet pressure (psig), P bonnet.--125 Downstream pressure (psig), P down 0 Valve Disk Geometry: hub radius, b:=4.94 meanseatradius, a:=5.75 averagediskthickness, t:=0.789 hub length, L:= 0.125 seat angle, a:= 7 1:= " a tt 2 180 e 0.061 Valve Disk Material Properties: 0 ishalfdisk'angle a modulus of elasticity, E:=29400000 Poisson's Ratio, v.=0.3 Other Valve Parameters: Valve Stem Diameter, D <~.--2 Static Unseating Thrust, F po 2129

                                                                     ¹ (reference: Test 11. SS96)

Valve Factor VF:=0.6 (reference: NER-2M-010) CALCULATIONS: cos(e) Coefficient of friction between disk and seat, p:=

                                                                '- s~(e)                  p   0.622     (reference    ¹6) up+ down                                  =71 Average DP Across Disk,                 avg 'onnet                  2 gives,     DP Disk SINnes Constants, Et             Bed        G:=       E n(1    -')                           2 (1+v) which gives,      D =1.322     10         and          G =1.131 ~ 10 GeometryFactors, 4,a C2.=

1 b 1+2 1n a

b C3'.=. b 4a b

                                                                                        +1 a

ht a

b b

                                                                                                         +  -1 a

C8 =-1 2 1+ v+(1 v) b a 2 C9 a 1-

                                                                               --b 1+v2 a

ln + b 1-v 4 b a 2 which gives, C 2 =0.009 C3 =4.316'10 C8 0.908 C 9 ~0.124 COMED PL Evaluation Valve ID: 2SWP'MOV18B page 1 PSWP18BA.MCD

r7 I if I I

Niagara Mohawk Power Corporation NMP2 Pagw'o//37 Nuctear Engineering Calculation Cont. Sheet A10.1-AD403, RW, 01 Checker/Oate Originator/Date Q~~~ o 4 - C~ &2j/5 7 ~~/./~r Additional Geometry'Factors, rp .'=b 2 4 2 2 I I+4 -5 rp fp 4 fp 2+ In-rp a 64 a a a a rp L17 I 4 I - I-1-Y 4

a 4 a 0 2 I +(I+ Y) In a rp which gives, L 11 =1.545 10, and L17 =0.009 Moment Factors, Mrb' DP avg a Cg C9 2ab

a -rp -L17 Qb'a 2b

                                                                                                              -r0 j which gives, M+--25.298                   and            Qb-62.225 Deflect/on from pressure/t/ending, 4
                             .'=Mrb 3

avg a C2+Qb C3-a a yb D D D LII which gives, yb q =-3.016 10 Deflection fiom pressure/shear, 2 K ~:=-0.3 2 In a I + rp

2 I 2 In-brp sa'vg a b a ysq'hich gives, K sa ~.013 and y" ~-3.297 10 s sq Deflection from pressure/hub stretch, P f tt (a b ) DP g y stretch 'b P force'L 2E which gives, force

                                                                    '                            y~<<h      -5355'10 COMED PL Evaluation                               Valve ID: 2SWP MOV18B                                                      page 2 PSWP18BA,MCD                                                                                                                   ~i

Niagara Mohawk Power Corporation NMP2 Pager"trot /7 7 Nuctear Engineering Calculation Cont Sheet A10.1-AD403, Rev. 01 Originator/Date Checker/Date R~pju W P~~ ~fg+g7 ~~/slur Total Deflection due to pressure, yq 'bq+ysq+ystretch which gives, y q =%.367.10 Additional Geometry'Factors ro'.=a L3 '.= ro 4a ro a 2 1-1 ~ In + - I r a ro a 2 L9.= a

ro I+v 2 In a ro

I-v 4 I ro a 2 which gives,'" L3 ~0 and 'L9 ~0 Deflection from seat load/bending, w:= I y bw ..=- D C2 C8 roC9.- b L9 roC3 b

                                                               + L3     which gives,        yb       1437 10
                                                                                                                'r Deflection from seat load/sheer, Ksa:=-1.2 ro ro

a In-b y sw'G

                                                   .'=Ksa            which gives,           Ksa ~ %.182 y ~   -1.174 10 Deflection from seat load/hub compression, L
                          -2tta      2 which gives,                        ~ I'002 10 y compr '                                                       ycompr itb Total Deflection from unit seat load, yw:=ybw+ysw+ycompr                             which gives,           y w -2.621 ~ 10 Equilibrium contact load distributr'on, w eqmlibri~      'hich yq yw gives,       w equilibrium = 24.291 Load per seat =           2 tt.a yq     877.591 yw Pressure LocMng Force, COMED PL Evaluation                               Valve ID: 2SWP'MOV18B                                              page 3 PSWP18BA.MCD

f' NMP2 PageirSot/3 ~ Niagara Mohawk Power Corporaaon Nuotear Engineering Catoulation Cont. Sheet A10.1-AD403, Rev. 01 CheckerlDate

                                                              ~io.rrrW F pres lock:=

1 2 tt a Yq (p cos(0) - sin(0)) 2 which gives, F pres lock 981 925 W Piston Effect Force, . P au:=0

                        '=                          p stm)           which givess    F lston off~e    392.699 "piston street S'D stem '(p bonnet "Reverse Piston Effect" Force, Fvert'=     rt a   2Pbonnet        up      down which gives,      F ~ = 900.428 Total Force Re uired to Overcome Pressure Lockin
              '                         F         F pist F total       pres lock+ F po + veft
                                              '                              '

which gives, <<~ =3.618654 10 ACTUATOR CAPABILITY: Actuator Model/Size: = SMB-0-25 Motor Torque Output: TQm:= 23.52 ft- Ibs Gear Ratio: OGR:= 39.11 Application Factor. Af:=0.9 Pullout Efficiency: Eff:=0.4 Reduced Voltage: RV:=0.8852 Torque Output: TQout:= Tg RV OGR Afar TQout = 259.484 tt- lbs Stem Factor. St: = 0.019627 Thrust Capability: THcap .'= TQout Sf THcap ~ 1.322 10 lbs NOTE: RV IS SQUARE IF ACTUATOR IS AC. ENHANCED PRESSURE LOCIQNG METHODOLOGY: KEI:= 1.20 Thrust Msrtpn:= THeep (Fmmt KEI) Thrust Margin ~ 8.878'10 lbs I

Conclusion:

Open Thrust Margin is positive, therefore this valve and actuator are likely to overcome the theoretical pressure locking conditions evaluated. COMED PL Evaluation Valve ID: 2SWP'MOV1 8B page 4 PSWP18BA.MCD

0 Niagara Mohawk Power Corporation NMP2 Page C4or~ 7 Nuctear Engineering Calcutation Cont. Sheet A10.1.AD403, RW. 01 Originator/Date Checker/Date Q ~/~3bp ~vrzjt7 Valve ID no: 2SWP'MOV2tA Re uired 0 enin Force Deternmination under Pressure Lockin Conditions COMED Method DESIGN INPUTS: Design Basis Conditions at time of Pressure Locking Event: Upstream pressure (psig), P np 108 Valve Bonnet pressure (psig), P bonnet .= 2314 Downstream pressure (psig), P d ~.=0 Valve Disk Geometry: hub radius, b:=0.875 mean seat radius, a.=1.47 average disk thickness, t:=0.54 hub length, L:=0.25 seat angle, a.=10 .a e:=- tt e =0.087 2 180 Valve DIsk Materfai Properties: 0 ishalfdisk angle u modulus of elasticity, E;=29400000 Poisson's Ratio, v.=0.3 Other Valve Parameters: Valve Stem Diameter, D< .=1.125 Static Unseating Thrust, F o:=1890 (reference: Test ¹ 7, 3/30/93) Valve Factor VF:= I (reference.'ER-2M-010) CALCULATIONS: cope) Coefficient of friction between disk and seat,

                                                                  '- s~(e)               It =1.091     (reference    ¹6) up+ down                                         3 Average DP Across Disk,                 avg       bonnet                            gives,      DP avg    2 26 10 2

Disk SNfnes Constants, D:= Et and G:= E iz(i-') 2 (I+ v) which gives, D ~4.239 10 and G ~ 1.131 ~ 10 GeometryFactors, C2.=-I 4 I- b

a I+21n a b C3'.= 4a

a I In a

b

a

                                                                                                               -   I C8'.=-I 1+ v+(I- v) 2 b

a 2 C 9.=- I- In + which gives, C 2 =0.07 C 3 =0.008 C 8 0774 C 9 ~0.268 COMED PL Evaluation Valve ID: 2SWP MOV21A page 1 PSWP21AA.MCD

Niagara Mohawk Power CorPoration NMP2 Page C'Pot /7 7 Nuctear Engineering Catcutation Cont. Sheet A10.1-AD403, Rw. 01 Originator/Date Checker/Date so~.oy~ 4Q~ PZ)$ g Additional Geometry Factors, rp .'=b 2 4 2 2 fp In-I 1+4 4 rp 5 rp rp 2+ ~ 64 a a a a rp L17 I 4 I - I- - 4 rp a 4 rp a 2 I +(I+v) In a rp which gives, L 11 =9.149 10 and L17 ~0.063 Moment Factors, M~'=- Dpavg C8 wh/ch g/ves, 2 C9 2ab (a -ro )-Lrr ~b:= 2b

                                                                                                  '"'(*-               0')

M rb =-516.898 and Qb 1.802 10'eflection f/Qm pressureIbending,

yb .=Mrb O C2+ 2 Qb C 3-D D

                                                                                   .L 11 which gives,               y bq ~%.158           10 Deflection from pressure        Ishear, 2                                                                   2 rp                                           avg a K ~:=-0.3 2 In  - I +

rp ~ I-2 In-b sa tG b a which gives, Ksa =%.118 a/ld y'sq = %.403'10 Deflection from pressure /hub stretch, P force'L P,:=a (a'- b') DP,, y stretch ttb 2E which gives, P force 9 906 18 and y stretch =-1.751. 10 COMED PL Evaluation Valve ID: 2SWP'MOV21A page 2 PSWP21AA.MCD

NMP2 Pagerr 1/o/~7 > Niagara Mohawk Power Corporation Nuclear Engineering Calculation Cont. Sheet 4 A10.1.AMX},Rw. 01 Originator/Date Checker/Date Row i>pc, A. Q~ QZy/p p ~/i/~r Total Deflection due to pressure, yq ' bq ~ y sq+ y.trctch which gives, y =-2.031 ~ 10 Additional Geometry Factors ro:=a L3 '= ro 4a ro a 2

                              +1  1n +  -1 a

ro ro a 2 ro a

L9.= 1+v 1n 2 a ro

1-v 1- ro 4 a 2 which gives, L3 =0 and L9 =0 II Detlection from seat load/bending, w:=1

y bw. a D w C2 C8 roC9 b L9 roC3 b

                                                             + L3     which gives,        ybw       64' Deflection from seat load/shear, Ksa:=-   1.2 ro ro a

1n-b y:=Ksa sw ' which gives, Ksa W.623

                                                                                           ~ ~-1:499'10 Deflection from seat load/hub compression, L

y compr 'b -2tta 2 which gives, y ~-1.633 10 Total Deflection from unit seat load, yw:=y bw+y sway compr which gives, yw 3.626 10 Equilibrium contact load distribution, w ~b-~.= yq which gives, w cquiTibrium 5%'241 yw Load per seat r 2 tt a yq 5.175 10 yw Pressure Locking Force, COMED PL Evaluation Valve ID: 2SWP'MOV21A page 3 PSWP21AAMGD

Niagara Mohawk Power Corporation NMP2 Page/ /of I$ 1 Nuctear Engineering Catcutation Cont. Sheet A10.1-AD403. Rev. 01 Originator/Date Checker/Date

          ,>; A'. a Pdislp~                                     Pio.rid Yq
                                 "                                                     F pres loc'k = 1 .035    0 4

F pres ]ocp 2 ft a ( p cos(0) sin(0)) 2 which gives, 1 W Piston Effect Force, Pat:=0 ft "piston etr(mt ' stem 'i bonnet p etm) which givesr F piston cff~t "Reverse Piston Effect" Force, v~:=" Pbonnct- up- so~ 'm<<) which gives, F crt = 2.674 10 Total Force Re uired to Overcome Pressure Lockin F total.'=Fprcs lock+ Fpo+'F vert Fpiston cffcct

which gives, <<~ =1.261328 10 ACTUATOR CAPABILITY: Actuator Mode! I Size: = SMB-000-5 Motor Torque Output: TQm .'=4.76 ft- 1bs Gear Ratio: OGR:=52 Application Factor. Af:=0.9 Pullout Efficiency: Eff:=0.4 Reduced Voltage: RV:= 0.8623 Torque Output: TQout:= TQm RV OGR AfEff TQout ~ 66.257 ft- lbs Stem Factor. Sf:= 0.014500 T TQoutut Thrust Capability: fHcap:=. THcap ~4.569 10 lbs Sf NOTE: RV IS SQUARE IF ACTUATOR IS AC. ENHANCED PRESSURE LOCNNG METHODOLOGY: KEI:= 1.20

                   'ibrnst Mer(pn:= THeep- (FmmrKH1)

Thrust Margin ~-1.057 10 1bs

Conclusion:

Open Thrust Margin Is negative, therefore this valve and actuator are unlikely to overcome the theoretical pressure locking conditions evaluated. COMED PL Evaluation Valve ID: 2SWP'MOV21A page 4 PSWP21AA.MCD

NIagara Mohawk Power CorPoration Nuctear Engineering NMP2 Calcutation Cont Sheet Page7uor /97 A10.1-AD403, RW. 01 Originator/Date ~enie3w A. g e'/e3leg Checker/Date eke Valve ID no: 2SWP MOV21B Re uired 0 enin Force Defernminafion under Pressure Lockin Conditions COMED Method DESIGN INPUTS: Design Basis Conditions at time of Pressure Locking Event: Upstream pressure (psig), P :=108 Valve Bonnet pressure (psig), Pbo <<.=2314 Downstream pressure (psig), P do~ 0 Valve Disk Geometry: hub radius, b:=0.875 mean seat radius, a:=1.47 average disk thickness, t:=0.54 hub length, L:=0.25 seat angle, a.=10 0:=-a tt 2 180 0 0.087 Valve Disk Material Properties 0 ishalfdiskangle a modulus of elasticity, E:= 29400000 Poisson's Ratio, v:=0.3 Other Valve Parameters: Valve Stem Diameter, D <~.=1.125 Static Unseating Thrust, F po 1245 (reference: Test¹ 12, 1295) Valve Factor VF:= 1 (reference: NER-2M-010) CALCULA77ONS: Coefficient of friction between disk and seat, cos(0)

                                                                     - sin(0)              it =1.091      (reference    ¹6)

P~+Pdo~ Average DP Across Disk, D avg" bonnet gives, DP a2.26 10 2 Disk SNI'nes Constants, D:= Et3 end G:= 2 E (1+ v) which gives, D 4.239 10 and G = 1.131 ~ 10 GeometryFactors, C2.= 1 4 b a 1+2 1n a

b C3.= 4a b b2

                                                                                       +1 a

a ln + b b2

                                                                                                              -1 a

C8 '=- 1 2 1 + v+ (1 -, v) b a 2 a

C9.'=-b 1+v ln 2 a b

                                                                                                  + .1-1 4

v b a 2 which gives, C 2 =0.07 C 3 ~0.008 C 8 ~0.774 C 9 =0.268 COMED PL Evaluation Valve ID: 2SWP'MOV21 B page 1 PSWP21BA.MCD

Niagara Mohawk Power CorPoration NMP2 Pagey/ of/3 7 Nuclear Engineering Calculation Cont. Sheet At 0.t-AD403, Rev. 01 originator/Date Checker/Date Additional Geometry Factors, rp '.=b 2 4 2 2 1 1+4 rp

                               -5  4      rp            rp 2+    ln-rp          a 64             a              a             a               a         rp L17 1

4 I 1-Y 1-4

a 0 4 a 0 2 I+(1+ Y) ift a rp which gives, L 1 1 =9.149 10 and L17 ~0.063

Moment Factors, 2 DP ayg a 2ab 9 ~ a -rp -L17 ob:= 2b

                                                                                                    '"'('-     0')

C& which gives, Mrb -516.898 and Q b ~ 1.802'lp W Deflection from pressure&ending, yb rb'a o 2+Qb' o 3 DP ayg a o

                                                                                     'l which gives,                  y bq ~%.15&          10 Deflection from pressure /shear, I

K~:=-0.3 21n -1+ rp 2'

1-21n-

                                                                       'p                    '=

s'a'vg a 2 a b ysq which gives, K sa ~.l 1 & and y'.403 sq 10 Deflection from pressure/hub stretch, P force L P force tt (a b ) DP ayg y stretch '= itb 2E which gives, Pf0~ =9.906.10 and y~~ -1.751 ~ 10 COMED PL Evaluation Valve ID: 2SWP'MOV218 page 2 PS.WP21BA.MCD

0 Niagara Mohawk Power Corgoration NMP2 Page 72bi/77 Nuotear Engineering Catcutation Cont. Sheet A10.1-AD403, Rev. 01 Originator/Date >c ~p- 8'~ Wzp/pp Checkerloate Total Deflection due to pressure, yq '=ybq+ysq+ystretch which gives, yq 2 031 10 Additional Geometry'actors ro.'=a L3 '= ro 4a ro a 2

                                +   I In +

a ro ro -

a 2 I L9 "= a

ro I+v 2 ln a ro

I-v I-4 ro a 2 which gives, L3 ~0 and L9 ~0 Deflection from seat load/bending, w:=I

                                                   'sa
       ~          a3w C2 ro C9

roC3 =-1.964 7 y bw.-

L9 + L3 which gives, yb 10 D C8 b b Deflection from seat load/shear, Ksa:=- 1.2 ro ro

a In-b y:= sw Ksa which gives, ~ W.623 y sw ~-1.499 10 Deflection from seat load/hub compression, L

                           - 2'1t'a   2 y compr
                       'tb                       which gives,               y       ~-1.633 10 Total Deflection from unit seat load, y w:=y bw+'y sway compr                         which gives,           y w ~-3.626'10 Equilibnum contact load distribution,
                                '

yq which gives, w equilibrium 560'241 equilibrium yw Load perseat= 2 tt a yq ~5.175 10 yw Pressure Locking Force, COMED PL Evaluation Valve ID: 2SWP'MOV21 B page 3 PSWP21BA.MCD

I NMP2 Pa//el &o/ I >> Niagara Mohawk Power Corporation Nuotear Ent/ineeriny Catoutatton Cont. Sheet A10.1-AD403, Rev. 01 Onglnatof/Date Checker/Date wowrop A ' /r(gSrp7 ~re rtr+p F pres loca '= 2 tt a J tl (P cos(e) sin(e)) 2 which gives, F, 1~1, 1.035 10

                               >w Piston Effect Force,                           P  at:=0 P piston pt on etreet
                        '=

4

                             'tern   '(P ttonnet   P ann)           which gives,         P piston street "Reverse Piston Effect" Force, vert onnet                   up      down which gives,           F ~     2.674 10 Total Force Re uired to Overcome Pressure Lockin F totai: = F pres loca + F po+ F vert- F piston effect which gives,        F <<nd =1.196828 10
                                                                            'CTUATOR CAPABILITY:

Actuator Model/Size: = SMB-000.5 Motor Torque Output: TQm;=4.76 ft- 1bs Gear Ratio: OGR:=52 Application Factor. Af:=0.9 Pullout Efficiency: Eff:=0.4 Reduced Voltage: RV: = 0.8591 Torque Output: TQout:= TQm RV OGR AfEff TQout = 65.766 ft- lbs Stem Factor: Thrust Capability: THcap: =TQout Sf Sf:= 0.014500 THcap =4.536 1(P lbs NOTE: RV IS SQUARE IF ACTUATOR IS AC. ENHANCED PRESSURE LOCNNG METHODOLOGY: KEI:"

                                                                                         -1.20 Thntat Margin:= THcap  (F tong KEi)

Thrust Margin ~%.826'10 1bs

Conclusion:

Open Thrust Margin Is negative, therefore this valve and actuator are unlikely to oVercome the theoretical pressure locking conditions evaluated. COMED PL Evaluation Valve ID: 2SWP MOV21B page 4 PSWP21BA.MCD

Niagara Mohawk Power Corporatke NMP2 Calcukrtion Cont. Sheet Page7rtor/ pp Nuciear Enginoerinp A10.1-AD403, Rev. 01 Orlglnatof/Data CheckerlDate Qo nv rp> A tot s /s p lng .

                                                                             ~re/r7 Valve ID no: 2SWP MOV66A Re uiredO enin                  ForceDeternminationunderPressureLockin                                               Conditions COMED Method DESIGN INPUTS:

Design Basis Conditions at time of Pressure Locking Event: I Upstream pressure (psig), F := 108 Valve Bonnet pressure (psig), P b <

                                                                                                                  = 108 I

Downstream pressure (psig), F go~ 0 Valve Disk Geometry: hub radius, b:= 3.375 mean seat radius, a:= 3.91 average disk thickness, t:=0.48 hub length, L:=0.125 seat angle, a:= 10 e:= a tt

2 180 e 0.087 Valve Disk Material Properties: e is half disk'angle a of elasticity, E:= 29400000'odulus Poisson's Ratio, v.'=0.3 Other Valve Parameters: Valve Stem Diameter, D ~.= 1.625 Static Unseating Thrust F po 9232

                                                                             ¹ (reference: Test 25, 10/5/94)

Valve Factor VF:=0.65 (reference: NER-2M-010) CA L CULA77ONS: Coel'cient of fnction between disk and seat, It:=

VF I am(e) It =0.686 (reference ¹6) Average DP Across Disk, DP avg ' Fup+F de gives, DP avg 54 Disk Etttthss Constsnts, D:= Et snd G:= E tk (t s') 2(tsv) which gives, D 2.977'10 and G =1.131 ~ 10 Geometry Factors, C 2.'=-I 4 I - b

a I <<2 In a b C3.- + I In + - I C8 .'=-I 2 I+ v+ ( I - v) b a C9 -- I-In + which gives, C2 0.009 C 3 =3.965'10 C 8 ~0.911 C 9 = 0.121 (o+ COMED Pi Evaluation Valve ID: 2SWP'MOVS48 page 1 PSWP66AA.MCD

Niapara Mohawk Power Corporation NMP2 Pape75 ot /77 Nuclear Enpineerinp Calculation Cont. Sheet A10.1 AO403. Rw. Ot Oripinator/Oate Checkerloate Q~~~ A'. g~ Wiplpp Addih'onel Geometry Factors, rp .'=b 2 4 2 2 fp fp

LII = I+4 -5 -4 fp fp ~ 2+ In 64 a a a a rp L17 I 4 I-I-U I - 4 a 0 4

a 0 2

I+(I+v) ln a rp which gives, L I I =1.378 10 and L 17 =0.009 Moment Factors, Mg:=- avg 2 9 /2

                                                    'o)                                              '"'a'- ra'j C8          2ab                                                            2b which gives, Mrb -8.373                   and             Qb-3118 Deflection from pressurelbending, 4

3 avga

                            .'=Mrb C2+Qb C3-a                    a yb              D                    D                   D LII which gives,                 y b tI -1.937 10 Deflection fmm pressure/sheer, 2                                                          2 K ~:=-0.3       2 In a

I + b rp a

I - 2 In- rp b sq'G Ksa DP av'g'a which gives, Ksa ~%.012 end y'1.796 sq 10 Deflection from pressure/hub stretch,

                                                                                             -P force L P f    '.=ll (a   - b ) DP      vg                         y stretch     '=

rtb 2E II which gives, and y ~tch -3.928 10 P f0~ 661.191 COMED PL Evaluation Valve ID: 2SWP'MOV66A page 2 PSWP66AA.MCD

Niagara Mohawk Power Cotporatton NMP2 Nuotear Enttineertntt Catoulation Cont. Sheet A10.1 AD403, Rw. 01 Orfttlnatorioate Checkerloate >~ ~~> A'.g~ c /gy+) 7/i/~y Total Deflection due to pressure, yq'bq+ysq+ystretch which gives, y q ~-3.77I'10 Additional Geometry Factors r0.'=a L3 .'= ro

4a ro a 2

                               +I    ln +  - I a

ro r0 a 2 r0 a I-L9.= 1+v In 2 a ro

I v 4 a 0 2 which gives, L3 =0 and L9 =0 Deflection from seat load/bending, w:= I ybw.= a.w C2 roC9 D C8 b L9 roC3 b

                                                              +L3 which gives,              ybw       1835 10 Deflection from seat load/shear, ro ro

Ksa:=-1.2 a ln- b y:=Ksa- tG a which gives, Ksa =-0.177 y =-I 272 10 Deflecflon from seat load/hub compression, L

                           -2 tt'a  2 compr   'tb                    which gives,                y          -1.459 10 Total Deflection from unit seat load, y w:=y bw+y sw+y compr                       which gives,             yw     3 122'10 Equilibrium contact load distribution, we    ~bn~.=        yq         which gives,              equilibrium    12'081 w

Load per seat = 2 a a yq 296.797 yw Pressure LDCMng Force, COMED PL Evaluallon Valve ID: 2SWP MOV66A pag8 3 PSWP66AA.MCD

0 Niagara Mohawk Power Corporation NMP2 PageTfo/ I +'7 Nuciear Engineeiing Ceioiglation Cont. Sheet A10.1-AD403. Rev. 01 4.~ Originator/Date Checker/Date a~"p" 4/go/pr

                                                          ~rs        r.r r/

F pres leak' tt a " Yq (p;cos(e)- sin(e)) 2 which gives, Fpres look =354.165 Vrr Piston Effect Force, Pau '=0 F piston street D stem 2/'(p bonnet p atm) which gives, F piston eff~t = 223.986 "Reverse Piston Effect" Force, F<<.'= it a 2 P bonnet up gown which gives, F v<< = 452.0SS Total Force Re uired to Overcome Pressure Lockin F total:=F pres look+ F po+ F v<<- F piston which gives, F +~ = 9.814267'10 ACTUATOR CAPABILITY: Actuator Mode)/Size: = SMB-00-15 Motor Torque Output: TQrn: = 14.74 ft- lbs Gear Ratio: OGR:= 34.1 Application Factor: Af:=0.9 Pullout Efficiency: Eff:=0.4 Reduced Voltage: RV:= 0.8838 Torque Output: TQout:= TQI RV OGR AfEff TQout = 141.339 ft- lbs Stem Factor: Sf:= 0.016407 Thrust Capability: THcap "= TQout Sf THeap = 8.615'10 Ibs NOTE: RV IS SQUARE IF ACTUATOR IS AC. ENHANCED PRESSURE LOCNNG METHODOLOGY: KEI:= 1.20 Throat Margin:= THoap (Fm~ Kgi) n Thrust Margin -3.163'10 lbs

Conclusion:

Open Thrust Margin ls negative, therefore this valve and actuator are likely to overcome the theoretical pressure locking conditions evaluated. 4 COMED PL Evaluation Valve ID: 2SWP'MOV66A page 4 PSWP66AA.MCD

ll Niagara Mohawk Power Corporation N ucteaf Engineering HMP2 Calculation Cont Sheet Page7+1 /37 A10.1.AD403, Rev. 01 Oflglnatof/Date Checker/Gate A 0$g cfs E i)7 ~/<C Valve ID no: 2SWP'MOV66B Re uired 0 enin Force Deternmination under Pressure Lockin Conditions COMED Method DESIGN INPUTS: Design Basis Conditions at time of Pressure Locking Event: Upstream pressure (psig), P>>.=108 Valve Bonnet pressure (psig), Pbo~ct -108 Downstream pressure (psig), P ~o~.=0 Valve Disk Geometry: hub radius, b:= 3.375 mean seat radius, a '.=3.91 average disk thickness, t:=0.48 hub length, L:=0.125 seat angle, a:=10 6:=-a tt 2 180 6 0.087 Valve Disk Material Properties: 6 ishalfdisk'angle u modulus of elasticity, E:=29400000 Poisson's Ratio, v.=0.3 Other Valve Parameters: Valve Stem Diameter, D <~.= 1.625 Static Unseating Thrust F 7027 po

                                                                        ¹ (reference: Test 16, 3N/94)

Valve Factor VF:=0.65 (reference: NER-2M-010) CALCULATIONS: cos(6) Coefficient of friction between disk and seat, It:=

VF I sitt(6) p 0.686 (reference ¹6) Pup+Pdo~ = 54 A~erage DP Across Disk, DP ayg: P boggct- gives, DP 2 Disk SNnves Censlsnls, D:= Et snd G:= E 12 (! - v ) 2 (! vv) which gives, D 2.977 10 and G = 1.131'10 Geometry Factors, C 2.=-I 4 I - b

a I + 2 ln a b C'3 .'.= b 4a b

a

I h a b

                                                                                                                 +  -

a I C8.'= I 2 I+ v+(I - v) b a C9 a

                                                                                   =-b 1+v In 2          b a
                                                                                                         +

I-v I-4 b a 2 which gives, C2 0.009 C 3 =3.965'10 C 8 ~0.911 C 9 ~0.121 COMED PL Evaluation Valve ID: 2SWPeMOVSICB page 1 PSWP66BA.MCD

I, Niagara Mohawk Power Corgoration NMP2 Page7?of /7 7 Nuctear Engineering Catcutation Cont. Sheet A10.1 AD403, Rw. 01 Checker/Date Originator/Date ~~ oPo W <~ ~M&7 ~/z/y y Add/t/onel Geometry Factors, rp.'=b 2 4 2 2 fp - fp - fp fp In L 11 '= 1 +4 5 a 4 2+ 64 a a a rp L17'.= I - I 4

I-Y 1-4 a 0 4

a 0 2

I+(I + Y) In rp a which gives, L I I =1.378 10 and L17 =0.009 Moment Factors, Mg:=- OP avg'a C8 2

                                ~  -rp C 9 2ab a                -L17                      ~b:=  , 2b
                                                                                                  '"'(*-    o*j which gives, Mrb =-8.373                end               Qb ~31.18 Deflection from pressureibending, 4

avg a 3

                           '.=Mrb C 2+ Q b C 3-a                    a yb                                                              L11 o                   o                  o which gives,               yb q ~ 1.937.10 Deflection from pressure         Ishear, 2

rp 2 rp sa'vg a K ~:=-0.3 2 In a

b

                                      - I+

a

                                                       ~     1- 2 In-b Sq'G which gives,              K sa =%.012                    end                y Sq  -1.796'10 Deflection from pressure/hub stretch,
                                                                                         -Pronx L Pro~.'=m (a      -b    ) DP~<                            >'uetch: =

ttb 2E 8 which gives, P fo~ = 661.191 end y~t h =-3.928 10 f COMED PL EvaluaIIon Valve ID: 2SWP MOV66B page 2 PSWP66BA.MCD

I Niagara Mohawk Power Corgoration NMP2 Page tourt /3 7 Nudear Engineering Calcuiation Cont. Sheet A10.1-AD403, Rw. 01 Originator/Date Checker/Date %~ryan~ Ai 4& 4'fdkpj ~p/z/rz Total Deflection due to pressure, yq y bq+ y sq+ y stretch y = -3.771 10

which gives, Additional Geometry Factors ro.'=a L3 .'= ro

4a ro a 2

                             + I In    +  - I a

ro ro a 2 L9 '.= a

ro 1+v 2

In a ro

I v 4 I ro a 2 which gives, L3 ~0 and L9 ~0 Deflection from seat load/bending, w:=1 ybw'9 a w C2 D C8 roC9 b

ro C3 b

                                                             +L3 which gives,              y bw =-1.835 10 Deflection from seat load/shear, Ksa .'=- 1.2 In-a ro b

y:=Ksa tG which gives, Ksa %.177 y~~-I:272 10 Deflection from seat load/hub compression, L y compr 'b - 2 "tt.a 2 which gives, y -1.459 10 Total Detlection from unit seat loa'd, yw' bw+ysw+ycompr which gives, yw 3122 10 Equilibrium contact load distribution, w e,l;b~. which gives, equilibrium yw Load per seat r- 2 tt a yq 296.797 yw Pressure Locking Force, COMED PL Evaluation Valve ID: 2SWP'MOV668 page 3 PSWP66BA.MCD

Niagara Mohawk Power Corporation NMP2 Page j/ot / W7 Nuotear Engineering CaCulati'on Cont. Sheet Atp.t-AD403, Rev. 01 Onglnstor/Date Checker/Date ~~ny u P- <5/g/as/P7 7 Fpres loci'.'= 2 tt a (it cos(e) sin(e)) 2 which gives, pres leak t W Piston Effect Force, P au:=0 "piston streettem 'i honest ann} which gives, F piston effect "Reverse Piston EIfect" Force, Fyert '= a' 2'P bonnet P up down which gives, F y~ = 452.088 Total Force Re uired to Overcome Pressure Lockin Ftptai t=F pres ]pck1 Fpp+ Fyert Fpistpn effect which gives, F tp< 7 609267 10 ACTUATOR CAPABILITY'ctuator Model ISize: = SMB-00-15 Motor Torque Output: TQm .'= 14.74 tt- lbs Gear Ratio: OGR:= 34.1 Application Factor: Af:=0.9 Pullout Efficiency: Eff:=0.4 Reduced Voltage: RV:-" 0.8847 Torque Output: TQout:= TQm RV .OGR AfEff TQout = 141.627 tt- lbs Stem Factor. Thrust Capability: THcap: = TQout Sf Sf:= 0.016407 THcap = 8.632 10 lbs NOTE: RV IS SQUARE IF ACTUATOR IS AC. ENHANCED PRESSURE LOCIQNG METHODOLOGY: KEI:= 1.20 Thrust Margin:= THoap- (Fmmt KEI) Y/cl'payee Thrust Margin -499.005 1bs

Conclusion:

Open Thrust Margin is negative, therefore this valve and actuator are likety to overcome the theoretical pressure locking conditions evaluated. ra/d4clcvat 4 J j 4 vdry mrrvelvlcr gt ptgsl 1'AdNC is a /rrglk cgpn/icPt~r.p pggp these'rpr lreertrresureroskio1 Seeeranro COMED PL Evaluation Valve ID: 2SWP'MOV66B page 4 PSWP66BA.MCD

Niagara Mohawk Power Corporation N)tctear Engtneerfng NMP2 calo)station Cont. Sheet Page~ /3$ A10.1-AD403, Rw. 01 Orfgtnatorloate Checker/Date g

                                                                               .
       ~~          A Q -tt>>/sv
                       ~

Valve ID no: 2SWP'MOV67A Re uired 0 enin Force Deternmination under Pressure Lockin Conditions COMED Method DESIGN INPUTS: Design Basis Conditions at time of Pressure Locking Event: Upstream pressure (psig), P up 108 Valve Bonnet pressure (psig), P bonnet = 108 Downstream pressure (pslg), P down 0 Valve Disk Geometry: hub radius, b:= 1.25 mean seat radius, a:=1.88 average disk thickness, t:=0.626 hub length, L:= 0.25 seat angle, a =10 e;=- u rt 2 180 e =0.087 Valve Disk Material Properties e is half disK angle a modulus of elasticity, E:=29400000 Poisson's Ratio, v:=0.3 Other Valve Parameters: Valve Stem Diameter, D st ..= 1.375 Static Unseating Thrust, F>> .= 2534 (reference: Tesr 10. ¹ 1M') Valve Factor VF:=1 (reference: NER-2M-010) CALCULATIONS: cos(0) CoeNicient of friction between disk and seat, it.=

                                                                              - sin(e)                  lt     1.091     (reference    ¹6) up ~     down Average DPAcross Disk,             '

=Pb gives, DP 54 Disk St)I)as ConstantsD:=

                                        ,
                                              ,andEt
                                              )s.()-s')

2 G:= 2 E (1+v) which gives, D 6.605 10 and G = 1.131 ~ 10 Geomet/yFactors, C2.= 1 4 b a 1+2ln a b C3 = b 4a b

                                                                                                     +1 a

h a b b

                                                                                                                         +  -1 a'

C8:=- 2 1 v+ b a 2 C 9,--b a

1+v ln 2 a b

1 4 v

                                                                                                                           ~ 1-   b a

2 which gives, C2 0.049 C 3 ~0.005 C 8 =0.805 C 9 =0.241 COMED PL Evaluation ID: 2SWP MOVQ48 @7'alve page 1 PSWP67AA.MCD

Niagara Mohawk Power Corporation NMP2 Pag ~bi yP Nuclear Engineering Calculation Cont. Sheet Ato.t-AD403, Rev. 01 Originator/Date Checker/Date Q~rwp o AiQrc44- 4rjQ3/pQ ~/4e Add/tional Geometry Factors, rp '=b 2 4 2 2 I rp rp rp rp 1+4. 5 -4 2+ 1n- a 64 a a a a rp L17 1 4 1 v 1-4 rp a 4

                                                 -   ro

a 2

1+ (1+ v) ln-a rp which gives, L11 4.481.10 and L 17 <0.046 Moment Factors, 2 avg a Mg:=- a -rp -L17 C8 2&b which gives, Mrb -13.186 and Q b =42.593 Deflection fmm pressure/bend/ng, 4

                              '.=Mrb C2+Qb
                                         &

C3-a avg'b L11 D D D which gives, yb ~-1.752'10 Deflection from pressure /shear, 2 2 K~:=-0.3 2.1n a 1+ rp

                                                         ~  1-    2 ln-brp                             sa'vg     a b             a                                                       t.G which gives,               K sa =%.078                    and                   y.    =-2.09 10 sq Deflection from pressu/8/hub stretch, P force  L Pfpree    tt (a      b ) DP avg                           y stretch '=

ttb 2E which gives, P fo~ 334.525 and y ~~ =-2.897'10 COMED PL Evaluation Valve ID: 2SWP'MOV67A page 2 PSWP67AA.MCD

I Niagara Mohawk Power Corporation NMP2 Page Pfotr 37 Nuclear Engineering Calculation Cont. Sheet A1 0.1-AD403, Rev. 01 Originator/Date CheckerlDate Qc~r.))~ 4. C'~ /g)(p-g Total Deflectr'on due to pressure, yq ' bq+ y sq + y stretch which gives, y -4.131 ~ 10 Additional Geometry Factors ro'.=a L3 '= ro 4a ro a 2

                               +I    In +  - I a

ro ro a 2 L9 - a

ro 1+v 2 In a ro

I-v I-4 ro a 2 which gives, L3 ~0 end L9 =0 Deflection from seat load/bending, w:= I ybw

              '-  a  w C2 roC9 D C8            b L9    roC3 b
                                                              + L3      which gives,         ybw Deflection from seat        load! shear, Ksa:=-1.2 ro ro

a In- b y ~:=Ksa a tG which gives, Ksa ~W.49 y sw ~-1.301 ~ IO Deflection fmm seat load/hub compression, L

                         -2tta      2 compr  'tb
                      .

E which gives, y compr Total Deflection from unit seat load, yw '=y bw+ysw+ ycompr which gives, yw ~ 2'868'10 Equilibrium contact load distribution, yq w equilibrium

                              'w              which gives,             equilibrium Load per seat        ra   2 tt a yq     170.165 yw Pressure Locking Force, COMED PL Evaluation                              Valve ID: 2SNIP'MOV67A                                            page 3 PSWP67AA.MCD

Niagara Mohawk Power Corporation NMP2 Pagano/ /7 /} Nuclear Engineering Catcutation Cont. Sheet At0.1.AO403. Rev. Ot Originatorlnate A. + /b/nslPP Checker/bate Yq F pres Jock tt'a'(tt'cos(e) sin(e)) 2 which gives, Fp~s 1~k

                                                                                                       =    0. 3 1'w Piston Effect Force,                          P  at:=0
                         tem '(

I 2 / which gives, F piston effect '160.368 piston effect bonnet etm}

 "Reverse Piston Effect" Force, F vert '= rt a  ~

2 P bonnet down sin(e) which gives, F v~ = 104.517 up Total Force Re uired to Overcome Pressure Lockin F totat:=F pres tock+ F po+ F vert- F piston effect which gives, F >~ =2.818478 10

                                                                           'CTUATOR CAPABILITY:

Actuator Model/Size: = SMB-000-5 Motor Torque Output: TQm '=5 ft- lbs Gear Ratio: OGR:=40 Application Factor: Af:=0.9 Pullout Efficiency: Eff:=0.4 Reduced Voltage: RV: = 0.8816 Torque Output: TQout:= TQm RV OGR AfEff TQout 55.96 ft- Ibs Stem Factor. Thrust Capability: THcap: =TQout Sf Sf': = 0.014263 THcap ~3.923 10 1bs NOTE: RV IS SQUARE IF ACTUATOR IS AC. ENHANCED PRESSURE LOCNNG METHODOLOGY: KEI:= 1.20 n M tp.:=nr p yt.~ffffi} Thrust Margin = 541.246 Ibs

Conclusion:

Open Thrust Margin is positive, therefore this valve and actuator are likely to overcome the theoretical pressure locking conditions evaluated. COMED PL Evaluation Valve ID: 2SWP'MOV67A page 4 PSWP67AA.MCD

0 Niagara Mohawk Power Corporation NMP2 peg+Car r3' Nudear Engineering Calcutation Cont. Sheet A1 0.1-AD403. Rw. 01 Originator/Date Checker/Date

>~i.p e A Q                           4,/tr/~7                                       7/</87 Valve ID no: 2SWP MOV67B Re      uiredo enin ForceDeternminationunderPressureLockin                                                         Conditions COMED Method DESIGN INPUTS'esign Basis Conditions at time of Pressure Locking Event:

Upstream pressure (psig), P>> .= 108 Valve Bonnet pressure (psig), P bonnet = 108 Downstream pressure (psig), P down 0 Valve Disk Geometry: hub radius, b:=1.25 mean seat radius, a:=1.88 average disk thickness, t:=0.626 hub length, L:=0.25 seat angle, a:= 10 e:=-a tt 2 180 e = 0.087 Valve Disk Material Properties: 0 ishalfdiskangle u modulus of elasticity, E:= 29400000 Poisson's Ratio, v.--0.3 Other Valve Parameters: Valve Stem Diameter, D< .=1.375 Static Unseating Thrust, F>>.=3092 (reference: Test 12, ¹ 10/1M4) Valve Factor VF:= I (reference: NER-2M-Of0) CALCULA77ONS: coge) Coeflicient of friction between disk and seat, p:=

                                                                       '- s~(e)               'lt    1.091    (reference    ¹6) 1    down up Average DP Acmss Disk,                   DP avg '      bonnet                             gives,     DP        =54 2

Disk StN'nes Constants, Et3 and G:= E i2(l-') 2 (I+ v) which gives, D 6.605 10 and G = 1.131 ~ 10 Geometry Factors, C2 '=-I 4 I -

a

I + 2 ln b C 3 .= b 4a b2

                                                                                            + I In a

a b

bi - I a c8:=-I 1+v+ 2 b a C9 -- - In + I b 2 which gives, C2 0.049 C 3 ~0.005 C 8 ~0.805 C 9 =0.241 COMED PL Evaluation Valve ID: 2SWP'MOVQ& page 1 PSWP67BA.MCD

Niagara Mohawk Power Corporation Nuclear Engineering NMP2 Calcutatton Cont. Sheet Page ~fr+7 A10.1-AD%03, Rev. 01 Originator/Date Checker/Date Qo~np~ A'-4~ ~ip/pp elitism AddtI'onal Geomehy Factors, rp.'=b 2 4 2 2 rp L I I:= I +4 5 - 4 rp rp rp ~ 2+ ~ In 64 a a a a rp L17 4 I I- I-v I - 4 ro a 4

                                                    -  ro a

2

I+(I + v) In a rp which gives, L11=4.481 ~ 10 and L 17 =0.046

Moment Factors, Mrb '=- OPavg' C8 2

                                       -rp)-LI7 2.a b r2
                                                '(a                                         ~b   =

2b

                                                                                                       '"'(*-    0*)

which gives, Mrb -13.186 and Q b =42.593 Deflectfon from pressure/bending, 2 avg a yb '=Mrb C2+ Qb a C 3- L11

                                         ,o                     o                o which gives,                      yb q        1752 10 Deflection from pressure/shear, Ksa'=-0.3        2.1n    a I+

r

2

I -2 In- rp m'vg a 2 b a b t.G which gives, K sa =%.078 arid y'sq =-2.09 10 Deflection from pressure /hub stretch, P force'L P fprce tt (a - b ) OP avg y stretch '= ttb 2E which gives, P f =334.525 and yst tch =-2.897 10 COMED PL Evaluation Valve ID: 2SWP'MOV67B page 2 PSWP67BA.MCD

Niagara Mohawk Power Corporation Nuoteer Engineering NMP2 Cetouletion Cont. Sheet Page $ hf /~ A10.1-A@003, Rev. 01 Originetotlnete goer gp o A 8~ g/r->lpga Total Deflection due to pressure, yq: ybq+ysq+y~~

                                                                                                     'I which gives,           y q =-4.131 ~ 10 Additional Geometry Factors r   .'=,a L3   .=

ro

4a ro a 2

                               +I   In r

a ro

                                            +  -I a

2 ro a

L9.'= . 1+v In 2

ro

I-v I-4 r0 a 2 which gives, L3 =0 and L9=0 Deflection from seat load/bending, w:= I a w C2 roC9 D CS b L9 roC3 b

                                                            + L3      which gives,        y bw      I'465'10    7 Deflection from seat load/shear, Ksa .'=-1.2 ro ro

a In- b y ~:= Ksa tG which gives, Ksa ~ W.49 y sw -1.301 10 Deflection from seat load/hub compression, L

                         - 2'1t'a  2 y compr '=                        which gives,               y        ~ "1.023 10 ttb     E Total Deflection from unit seat load, yw:=ybw+ysw+ ycompr                           which gives,          y w =-2.868    10 Equilibrium contact load distribution, w equilibrium ' yq              which gives,          w equilibrium     14 406 yw Load per seat =         2 tt a yq yw
                                               = 170.165 Pressure Locking Force, COMED PL Evaluation                           Valve ID: 2SWP'MOV67B                                                page 3 PSWP67BA.MCD

0 tl

Niagara Mohawk Power CorPoration NMP2 Catoutation Cont. Sheet Pagee j'o/ /37 Nuotear Engineering A10.1-AD403. Rev. 01 Checker/Date A+1 F pres 1lock

                      'w k:= 2 n a Yq (p cos(e) - sin(e)) 2          which gives,     Fpres lock
                                                                                                  = 3 0.3 Piston Effect Force,                           P  ~'.=0 F rara     airaar 'D     anan
                                      'P hennar    Fane)            whinh given F  pinna airaar i60368 "Reverse Piston Effect" Force, Fv~.=[en (gphe~ar-Pap-Pea~)]ain(8)                                 whi hngive a      F vm = 104.517 Total Force Re uired to Overcome Pressure Lockin "total  'res       lock+ po ~ vert          piston effect which gives,  '

3 376478 10 3. to< ACTUATOR CAPABILITYt Actuator Model/Size: = SMB-000-5 Motor Torque Output: TQm:= 5 lt- lbs Gear Ratio: OGR:=40 Application Factor. Af:=0.9 Pullout Efficiency: Eff:=0.4 Reduced Voltage: RV:= 0.8825 Torque Output: TQout:= TQm RV OGR.Af Eff TQout = 56.074 tt- lbs Stem Factor. Sf:-"0.014263 Thrust Capability: THcap .'= TQout Sf THcap ~ 3.931 ~ 10 lbs NOTE: RV IS SQUARE IF ACTUATOR IS AC. ENHANCED PRESSURE LOCKING METHODOLOGY: KEI:= 1.20 Threat Margin:= Tiicap (F n,ng.KEi) Thst Margin ~-120.34 lbs IL~

Conclusion:

Open Thrust Margin is negative, therefore this valve and actuator are likely to overcome the theoretical pressure locking conditions evaluated> Ayufetre 8 six r c Vle ieea~g p gn. ig go t./ns'e, ~et g~> ~fcms col'i egpecg4/ Ho >dr ev'. COMED PL Evaluation Valve ID: 2SWP'MOV67B page 4 PSWP67BA.MCD

Niagara Mohawk Power Corporation NMP2 Pager /P P Nuclear Engineering Calculation Cont. Sheet A10.1-AD403, Rev. 01 Checker/Date 'go~ ap n @ Q +l>%i&7 Valve ID no: 2SWP'MOV94A Re uired 0 enin Force Deternmination under Pressure Lockin Conditions COMED Method DESIGN INPUTSr Design Basis Conditions at time of Pressure Locking Event: Upstream pressure (psig), Valve Bonnet pressure (psig), P bonnet =108 P

                                         ~ .=10S Downstream pressure (psig), P down '=0 Valve Disk Geometry:

hub radius, b:= 3.375 mean seat radius, a:= 3.91 average disk thickness, t:=0.4S hub length, L:=0.125 seat angle, o:= 10 e =-a ft 2 180 e =0.087 Valve Disk Material Properties: e ishalf disk angle a modulus of elasticity, E:=29400000 Poisson's Ratio, v:=0.3 Other Valve Parameters: Valve Stem Diameter, D <~.--1.625 Static Unseating Thrust, F~.=7751

                                                                          ¹ (reference: Test 26, $ 9i95)

Valve Factor VF:= 0.65 (reference: NER-2M-010) CALCULATIONS: cos(e) Coefllcient of friction between disk and seat, p:= I VF

                                                                        - a~(e)               p     0.686    (reference     ¹6)
           ~+

up+ down Average DP Across Disk, DP avg ' bonnet gives, DP =54 2 Disk Stf'ffnes Constants, Et and G:= E u (i .*) 2 (1+ v) which gives, Geometry Factors, D C 2.977 10 2.=-I 4 I - b

a and 1 +2 ln b a, G = 1.131 ~ 10 C3.'= b 4a b

a

                                                                                              +   I In a

b

b a

                                                                                                                    -   I C 8.=-I 2

I+ v+ (I - v) b a a

C9.--b I+v In 2 b a

+ .

I-v I-4 b a 2 whichgives, C2 0.009 C3 =3.965'10 C8 0.911 C 9 <0.121 A COMED PL EvalUation Valve lD: 2SWP'MOV page 1 PSWP94AA.MCD

Jl 0

Niagara Mohawk Power Corporation NMP2 Page ~fo/r %~ Nuclear Engineering Calculation Cont. Sheet

                                                                                                               , A10.1&D40S. Rev. 01 Originator/Date cQ~~~+z            4'~           &/z 3j5p Checker/Date Additional Geometry Factors,                                 rp,=b 2             4              2                2
                            'o                           'o L11'=  1+ 4  -5  -4 ro                              ro 64 2+               ln- a a              a             a                 a           rp
                  '0 L17 4

1

1- 1-U 1-4 a 0 4

a 0 2

11-(1+ Y) 1n a rp which gives, L11 =1.378.10 and L 17 =0.009 Moment Factors, 2 Mrb DPavga C9 I 2 j

                                                                                                    '"'(*- 0*)

C8 2ab 2b which gives, M rb =-8.373 and Q b = 31.18 Dellection from pressureIbending, 4 DP avg a yb '.=Mrb C2+Qb' a C3- .L11 D D D which gives, yb q 1937 10 Deflection from pressure /shear, 2 .2 K~:=-0.3 21n a b 1+ rp 1-21n- rp ysq

                                                                                              '=    sa tG avg a a                   b which gives,               K sa =%.012                  .and                 y.

sq

                                                                                                    ~-L796   10 Deflect/on from pressure /hub stretch, P force  L Pforce'.=tt (a   -b     ) DPavg                          y stretch    =

nb 2E which gives, P force ~661.191 and y stretch -3.928'10 COMED PL Evaluation Valve lD: 2SWP'MOV94A page 2 PSWP94AA.MCD

                                                                                                                       /~/'3 7
                                                                          ~

Niagara Mohawk Power Cotporauon NMP2 Page Nuclear Engineering Calculation Cont. Sheet Ato.t-AD403, Rev. 01 Orlginatorlnate chackarlDste

                                                                                   ~/g/rr cCiygpg Total Deflection due to pressure,                          yq'bq+ ysq+ystretch which gives,           y q =-3.771 ~ 10 Additional Geometry Factors ro:=a L3   '=  ro
                 .

48 ro 8 2

                                +I    ln +  - I a

ro ro a 2 L9 - a

ro I+v 2 ln a ro

I-v I-4 a o 1 which gives, L3 ~0 and L9 =0 Deflection from seat load/bending, Wi= I ybw.'= 8 w C2 roC9 D C8 b L9

                                                  - roC3 + L3 b

which gives, y bw =-1.835'10 7 Deflection from seat load/shear, ro ro Ksa .'=-1.2 In-b y~.--Ksa- 8 which gives, Ksa = %.177 a tG y sw = -1.272'10 Deflection from seat load/hub compression, L

                          -2  tt.a  2 y compr
                        'tb                      which gives,              y compr

'otal Deflection from unit seat load, y w:=y bw+'y sw+y compr which gives, yw 3122 10 Equilibrium contact load distributfon, yq w equilibrium

                             'w                which gives,            equi]ibrium Load per seat -     "2     tt a Jq  ~ 296.797 yw Pressure Locking Force, COMED PL Evaluation                              Valve lD: 2SWP'MOV94A                                            page 3 PSWP94AA.MCD

Niagara Mohawk Power Corfgoratfon Nucfear Engineering NMP2 Catculation Cont. Sheet Page9+f /3 7 Atp.1 AD403, Rev. Ot t3rfginator/Date Checker/Date roy o Af ~ Q lfClgnlrp jgl rp It./ f/ F pres lock '= 2 ft a 1~ (it cos(6) - sin(0)) 2 which gives, F pres lock = 354.165 Yw Piston Effect Force, P an:=0 ft piston effect 'tem 'i bonnet p atm) which gives, F tstpn ~~t 223 986 "Reverse Piston Effect" Force, F veft a a 2 P bonnet P up P down sm(1) which gives, F ~ = 452.088 Total Force Re uired to Overcome Pressure Lockin F <<tal: = F pres lock+ F + F veft - F piston effect pp which gives, F <<~ =8.333267 10

                                                                              'CTUATOR CAPABILITY:

Actuator Model!Size: = SMB-00-15 Motor Torque Output: TQm '.= 14.74 tt- lbs Gear Ratio: OGR:=34.1 Application Factor: Af:=0.9 Pullout Efficiency: Eff:=0.4 Reduced Voltage: RV:= 1.0 Torque Output: TQout:= TQm RV OGR AfEff TQout ~ 180.948 ft- lbs Stem Factor. Thrust Capability: THcap: =TQout Sf Sf:= 0.016407 THcap = 1.103 10 lbs NOTE: RV IS SQUARE IF ACTUATORIS AC. ENHANCED PRESSURE LOCNNG METHODOLOGY: KE[:= 1.20 Thrust Margin: = THcap (F m~ KEI) Thust Margin ~ 1.029 10 1bs

Conclusion:

Open Thrust Margin ls positive, therefore this valve and actuator are likely to overcome the theoretical pressure locking conditions evaluated. COMED PL Evaluation Valve lD: 2SWP MOV94A page 4 PSWP94AA.MCD

Niagara Mohawk Power Corporation Nuclear Engineering NMP2 Calculation Cont. Sheet

>>

Pag~of / 5'7 A10.1.AD403, Rev. 01 > ~. p.. 4- Q~/iabp Originator/Date CheckeriDate r/s/N7 Valve ID no: 2SlrrVP'MOV94B Re uired 0 enin Force Oeternminafion under Pressure Lockin Condifions COMED Method DESIGN INPUTS: Design Basis Conditions at tIme of Pressure Locking Event: Upstream pressure (psig), P .=108 Valve Bonnet pressure (psig), P bonnet" 108 p Downstream pressure (psig), P down 0 Valve Disk Geometry: hub radius, b:=3.375 mean seat radius, a '.=3.91 average disk thickness, t:=0.48 hub length, L:=0.125 seat angle, a --10 0:=-.a rt 0 0.087 2 180 Valve. Disk Material Properties: 8 ishalfdiskangle a modulus of elasticity, E:=29400000 Poisson's Ratio, v.=0.3 Other Valve Parameters: hl Valve Stem Diameter, Dz .'=1.625 Static Unseating Thrust, F po 8674

                                                                           ¹ (reference: Test 6, tV1M3)

Valve Factor VF:= 0.65 (reference: NER-2M-010) CALCULA77ONSi CoeNicient of fnction between disk and seat, p:= cue)

                                                                          - sin(0)                p     0.686     (reference   ¹6) up+ down Average DP Across Disk,                   avg 'onnet"                    2 gives,     DP         =54 Disk Stiffnes Constants, Et              Sfl(t        G:=       E r2 (r    ')                            2 (1+v) which gives,       D =2.977     10        and            G      1.131 ~ 10 GeometiyFactors,           C2.'=-1 1-4 b

a 1+2ln a b C3.'=. b 4a b

                                                                                               +1 a

h a b

C8:=- 1 2 1+ v+(1- v) b a a

+-

C9.--.b 1+v ln 2 b a 1 4 v which gives, C2 0.009 C3 =3.965'10 C8 0.911 C 9 =0.)21 COMED PL Evaluation Valve ID: 2SWP MOV94B page 1 PSWP94BA.MCD

r~'7

Niagara Mohawk Power Corgoration NMP2 Page95of Nuclear Engineering Calculation Cont. Sheet A10.1 AO403, RW. 01 akkkkklrakrk Originatorloate ~~pc, Q. g~ ~gyypp 7/a/r7 Additional Geometry Factors, rp ',=b 2 4 2 2 L 11 '= I+4 rp - 5 rp

                                                   -4       rp        ~

2+ rp In 64 a a a a rp I-4 2 L 17 .'=-I I-v I- 0 rp ~ I +(I+ v) ln- a 4 4 ~ a a rp which gives, LII 1.378 10 and L 17 =0.009 Moment Factors, 2 Mg:=- DP avg a a -rp -L17 '"'(*- 0*) C8 2ab 2b which gives, M* -8.373 and Q b ~31.18 Deflection from pressure/bending, r 4 avg a 2+ Q b C 3 a a yb '.= M rb' C L 11 D O O which gives, yb, q

                                                       ~-I 937           10 Deflection from pressure/shear, 2                                                         2 rp                      Km.DP avg    a K ~:=-0.3 2 In a

I+ rp ~ I - 2 In-b t.G b a which gives, K~ ~%.012 and y sq -1.796'10 Deflection from pressure! hub stretch, P force'L

                                   -b Pra~.'=a    (a            ) DPak<                             y stretch
                                                                                          'tb      2E which gives,                 P f0~'"~ 661.191                      and       y stretch =-3.928 10 COMED PL Evaluation                                  Valve ID: 2SWP'MOV948                                                    page 2 PSWP94BA,MCD

1 I'I

A'MP2 ~ Niagara Mohawk Power Corporation N uotear Engineering Originator/Date ~reap g, Calcuiation Cont. Sheet cweaea as<a Page94efi' A10.1-AD402. Rev. 01 P Total Deflection due to pressure, yq'bq+ysq+ystretch y =-3.771 10

which gives, Additional Geometer Factors r:=a L3 '= ro 4a ro a 2

                                +  I  In +  - I a

ro ro a 2 L9 .= . a

ro I+v 2 ln a ro

1- v I-4 ro a 2 which gives, L3 =0 and L9=0 Deflection fmm seat load/bending, w:=I

                                                    'sa a  w C2 roC9                       roC3 ybw:=                               -L9                +L3 whichgives                ybw ~-1.835    10 D C8             b                  b Deflection from seat load/shear, Ksa:=- 1.2 ro ro

a ln- b y:= sw Ksa a which gives, ~ %.177 y sw ~-1.272.10 Deflection from seat load/hub compression, L

                            -2'tt a 2 compr   'tb                      which gives,                 y compr Total Detlection from unit seat load, yw:=y bw+ysw+ycompr                             which gives,            yw     3.122 10 Equilibrium contact load distnbution,
                    ~bn~ .'=

we yq which gives, w equilibrium 12.081 yw Load per seat >>- 2 tt a yq ~296.797 yw Pressure Locking Force, COMED PL Evaluation Valve ID: 2SWP'MOV94B page 3 PSWP94BA.MCD

Niagara Mohawk Power CorPoration NMP2 Pagerr/of J9 ~ Nucfear Engineering Cafcufation Cont. Sheet A10,1.AD403, Rev. Ot Onginator/Date Checker/Date wo~rzp rr ~ rob /p'/zs jpQ

                                                                             .ir/fCj7 Yq 2.,     q
                                      .(.~>0)         <0)).2         whichgives,             Fp        1~k=354   165 Yw Piston Effect Force,                            Pat:=0 piston  street
                          D         2  /p stem '(Pbonnet     Pstm)           wh/ch give~,

s F p,.st,n cff~t =223.986 "Reverse Piston Effect" Force, Fcrt.'-. ft a 2 Pbonnct- Pup- P flown sin(8) which gives, F v~ = 452.088 Total Force Re uired to Overcome Pressure Lockin

               .'=F F tptat       pres   loci'+ Fpc+ F vert- F piston cffcc which gives,        Ft  ~      9.256267'10
                                                                                'CTUATOR CAPABILITY:

Actuator Model/Sizar = SMB-00-15 Motor Torque Output: TQm ',= 14.74 ft- lbs Gear Ratio: OGR:= 34.1 Application Factor: Af:=0.9 Pullout Efficiency: Eff '=0.4 Reduced Voltage: RV:= 1.0 Torque Output: TQout:= TQm RV OGR AfEff TQout ~ 180.948 ft- lbs Stem factor. Sf:= 0.016407 TQout Thrust Capability: THcap: = Sf THcap = 1.103'10 1bs NOTE: RVIS SQUARE IF ACTUATOR IS AC. ENHANCED PRESSURE LOCNNG METHODOLOGY: KEI:= 1.20 Tbrnst Msrttin = THcsp - (F tomt KEI) Thrust Margin ~-78.799 1bs Qt/1

Conclusion:

Open Thrust Margin Is negative, therefore this valve and actuator are likely to . overcomethetheoreticalpressurelocklngconditlonsevaluated> pe~ever HAe rr/a~giw/~ ao girasol graf Hriis r/d/'~pgaep~ 4)drifts~ < ~4 COMED PL Evaluation Valve ID: 2SWP'MOV94B page 4 PSWP94BA.MCD

hl Y NlAGARA H Q MOHg~K .. CALCULATIONCONTINUATION'SHEET Page (Next ~at NUCLEAR ENGINEERING Nine Mile Point Nuclear Station Unit: 2 Disposition: NA Originator/Date cgiOWWP' ffe ~ ggP Checker/Date ria/~r A10.1-AD-003 Revision 01 ATTACHMENTS

                                                                           ¹ FORMAT NEP-DES-08, Rev. 01 (F02)

CACCldll/0>: A/0, (-AD a&9 P gv' ( NIAG&M IITOHAWK AA sl ~ed/ g NUcr.Em NG~~G

                                       ~~ ~Ay ~ P gg NOTES OF TELEPHONE CONVERSATION Persons Involved:           NMPC:               Gaines Bruce Anchor/Darling:     Ron Brubaker Date of Conversation:      Tuesday, August 22, 1995            2:45PM

Subject:

Internal Valve Dimensions for 2CSH*MOV101 Summary of Conversation: Ron called to state that he was working on our P.Q. to provide internal valve dimensions. Ron stated that as I had previously requested, that he was calling to provide me the dimensions for 2CSH~MOV101 in advance of the formal response. Applicable dimensions for 2CSH*MOV101 are: Seat OD: 13 1/2 inches Seat ID: 11 inches Hub Diameter: 4 inches Wedge angle: 6 degrees (includes both faces) Top of disc width: 2.013 inches Bottom of disk width: I/306 inches P/, Pod ") Hub width: 3/16 inch Ron stated that there was about 1/8 inch of hard facing on the disc scat. I advised him that I thought that MPR wanted thc width less hard facing. Ron'also stated that the hub width was not a uniform width from top to bottom. The sides are abrasive cut and that is the 3/16 inch dimension. Ron stated that he would try ta clarify what is being provided in the formal response. Action Required and Due Dates: No specific actions are to result f'rom this discussion. Anchor Darling is to,comply with P.O. Commitments: N/A xc: Ron Brubaker (by fax)

0 Niagara Mohawk Power Corporation Veian P.O. P9-80572 K DM-0050 Dimensional Data for Pressure Locking Analysis cP Velan Seat Dimensions Hub Hub Top of Disk Bottom of Disk Wedge Bonnet 0 Valve ID Dw . No. item Size OO ID Dia. Width Thick"ess Thickness An le Volume 2RHSA MOV112 P2-7026- N13 49 20 17.625 15.935 1<.250 0,37K %6/ 1.330 10 4464.7 2RHS*MOV113 P2-7026- N13 48 20 17.625 15.935 i 4.250 0 .375 1.330 10 4464.7 2RHS*MOV1 5A P3-7026-N10 47 16 15.906 14.906 1'..500 0.~00 ".~BP 1.406 10 3238.9 2RHS*MOV1 5B P3-7026- N10 47 16 15.906 14.906 i1.500 0.600 3.882 1.406 10 3238.9 2RHS*MOV25A P3-7026-N10 47 16 15.906 14.906 11.500 0.500 1.882 1.406 10 3238.9 2RHS*MOV2sB P3-7028-N10 47 16 15.906 14.906 11.500 0.600 1.882 1.406 10 3238.9 2SWP'MOV21A P3-7026- N18 62 3.125 2.760 1.750 0.500 0.528 0.552 10 639 2SWP*MOV21 B P3-7026- N18 62 3.125 2.760 1.750 0.500 0.528 0.552 10 63.9 2CSL4 MOV107 P3-7026- N2 13 3.938 3.576 2.500 0.500 0.628 0.624 10 111.0 2SWPA MOY67A P3-7026- N18 77 3.938 3.576 2.500 0.500 0.628 0.624 10 111.0 2SWP*MOV67B P3-7026-N18 77 3.938 3.576 2,500 0.500 0.628 0.624 10 111 0 2ICS*MOV129 P3-7026- N2 24 6.250 5.750 4.500 0.250 0.412 0.343 7 215.3 2ICS*MOV136 P3-7026-N2 24 6.250- 5.750 4.500 0.250 0.412 0.343 7 216.3 2HH8'OV4A P3-7028- N2 26 8.260 6.760 4.600 0.260 0.412 0.343 7 2163 2RHS*MOV4B P3-7026- N2 25 6 6.250 5.750 4.500 0.250 0.412 0.343 7 21s3 2RHS*MOV4C P3-7026- N2 25 6 6.250 5.750 4.500 0.250 0.412 0.343 7 215.3 2SWP*MOV66A P3-7026-N6 65 8 8.063 7.563 6.750 0.250 0.471 0.478 10 434.3 2SWP*MOV66B P3-7026-N6 65 8 8.063 7.563 6.750 0.250 0.471 0.478 10 434.8 2SWP'MOV94A P3-7026- N6 66 8 8.063 7.563 6.750 0.250 0.471 0.478 10 434.8 2SWP*MOV94B P3-7026-N6 66 8 8.063 7.563 6.750 0.250 0.471 0.478 10 434.8 2SWP*MOV17A P3-7026- N6 37 12 11.750 11.250 9.875 0,250 0.671 0.906 7 1294 0 2SWPo MOV17B P3-7026- NB 37 12 ii.7s0 11.260 9.876 0.260 A P7< 0.906 7 1294.0 2SWP'MOV1 BA P3 7026-N6 38 12 11.750 11.250 9.875 0.250 9 67"- 0.906 7 1294.0 2SWP*MOV18B P3-7026- N6 38 12 11.750 11.250 9.875 0.250 0.906 7 129 .0 2RHS'MOV1 15 P3-7026- N6 46 16 15.906 14.906 11.500 0.500 1.882 1.406 10 3238.9 2RHS*MOV1 16 P3-7026= N6 45 16 15.906 14.906 11.500 0.500 1.882 1.406 10 . 3238.9 2ICS*MOV1 26 P3-7026- NB 30 6 5.875 5.332 3.000 1.000 1.000 1.123 10 283.4 2ICS*MOV122 P3-7026- N10 40 12 11.750 11.250 9.875 0.250 0.671 0.906 7 1294.0 2ICS~ MOV1 21 P2-7026- N17 36 10 8.750 8.030 6.125 0.375 0.826 1.197 10 617.2 2ICS*MOV128 P2-7026-N17 69 10 8.750 8.030 6.125 0.375 0.826 1.197 10 617.2 Note: Dimensions are ln inches. Prepared by: John McDougall 24/08/1995 Rev 1

' 4M ~M me.~ C P~qt cd=4 C z4 COMMONWEALTHEDISON COMPANY PRESSURE LOCKING TEST REPORT Brian D. Bunte, P.E. Commonwealth Edison Company John F. Kelly, P.E. RECTA Technologies, inc. ABSTRACT Pressuie Locking is a phenomena which can cause the unseating thrust for' gate ygye to increase dramatically from its typical static unseating thrust. This can result in the valve actuator having insufficient capability to open the valve. In addition, this can result in valve damage in cases where the actuator capability exceeds the valve structural limits. For these reasons, a proper understanding of the conditions which may cause pressure locking and thermal binding, as well as a methodology for predicting the unseating thrust for a pressure locked or thermally bound valve, are necessary, This report discusses the primary mechanisms which cause pressure locking. These include sudden depressurization of piping adjacent to the valve and pressurization of fluid trapped in the valve bonnet due to heat transfer. This report provides a methodology for calculating the unseating thrust for a'valve which is pressure locked. This report provides test data which demonstrates the accuracy of the calculation methodology. DESCRY"HON OF PRESSURE LOCKING PHENOMENA Pressure locking occurs when the bonnet cavity pressure of a gate valve exceeds the pressure on hgh sides of the valve disk. The two primary mechanisms that exist for pressure locking of gate valves are described below: This pressure locking mechanism occurs when a valve is pressurized from one side. Leakage past the valve scat will cause the fluid in the gate valve bonnet to pressurize to.,the pressure of the high pressure side of the valve disk. Depending on the leak-tightness of the valve seats, this pressurizatio process may take seconds or hours; however, it is extremely unlikely that the valve seat will be sufficiently leak tight to prevent this process from eventually occurring. If the source of pressure is suddenly removed, then prcssure in the bonnet valve will remain trapped. Ifthe valve is called upon to open before the bonnet pressure has decayed to the line pressure, then a pressure locking event occurs. e The'time needed for the bonnet pressure to decay is dependent on several factors including leak tightncss of valve seats and packing. In addition, when the bonnet fluid is at a high temperature or contains large amounts of air, the, bonnet pressure decays much more slowly due to the pressurizer effect. Apparent cases of pressure locking occurring up to a day after the pressure source is removed have been recorded. However, test data presented later in this report suggests that the bonnet pressure is likely to decay within one hour of the sudden depressurization event 3C-9 'UREG/CP-0152

0 'I 0

g44 iehwy~y C C ~~ c+ C2~ urring ~is type of pressure locking is likely to occur when pumps adjacent to closed valves shut off or when an event such as a LOCA causes pressure on one side of a valve to suddenly <<op <<f

~en     the initial differential pressure across the valve disk is sufficient to unseat the high pressure side disk from its seat, then the bonnet pressure following a sudden depressurization event is less than the bonnet pressure at the start of the event. The maximum pressure which can be trapped in the valve bonnet can be calculated by determining the differential pressure at which the valve disk will come back into contact with the valve seat. Until the disk to seat contact is re-established, the bonnet pressure will follow the.upstream side pressure.          This calculation has been developed by ComEd, but is not provided in this report due to constraints on length.

This pressure locking mechanism occurs when the valve bonnet cavity of a gate valve is filled with liquid that contains little or no air. Ifa heat source is applied to fluid in the valve bonnet cavity, then expansion of the fluid can cause pressure in the valve bonnet to dramatically increase. The heat source can be fluid in piping adjacent to the valve or external environmental conditions as might be encountered following a high energy line break. Pressurization rates of-20 psi/'F to 60 psi/'F have been recorded during special testing. However, pressurization rates of this nature require the following conditions to exist: the valve seats and pachng must be very leak tight ~ the heat source must provide a high heat transfer rate to the bonnet cavity fluid ~ no air can exist in the valve bonnet cavity, or the temperature rise in the valve bonnet cavity must be sufficient to cause the expanding fluid to collapse the air bubbles before the high pressurization rate can be achieved. PRESSURE LOCKING CALCULATION MEI'HODOLOGY

1. The valve disk is assumed to act as two ideal disks connected by a hub. The equations in reference 1 are assumed to conservatively model the actual load due to pressure forces, 2.. The coefBcient of friction between the valve, seat and disk is assumed to be the same under pressure locking conditions as it is under DP conditions.

NUREG/CP4152 3C-10

                                                               ~X~U4aa           KLb   K   A)i CQX       <o i k44~~h ~g~+            C
                                                                                         ~%  c.K   c'
                        'gn 'nputs are used in calculating the force required to unseat a pressure locked i

MOV:

 ~         sign  ~is   Pressure Conditions at the time of the pressure locking event.       This includes the upstream (PP, downstream (P~ g, and bonnet pressure (P~J.
 ~      Valve Disk Geometry. This includes the hub radius (b), hub length (L), mean seat radius
     ., (a), seat angle (8), and average disk thickness (t). Figure 1 below is provided, for further clarification. When the hub cross-section is not circular (e.g. many Westinghouse gate valve designs), then an effective hub radius which corresponds to a circle of equal area to the hub cross-sectional area should be used.
 ~ Valve Disk Material Properties.              This includes the modulus of elasticity (E) and the Poisson's ratio (r) for the disk base material.
 ~ Valve Stem Diameter II (D~
 ~ Static Unseating Thrust         (FP
 ~ Coefficient       of Friction between Disk and     Seat (p) 3C-11                              NUREG/CP-0152

0 FIGURE 1 VALVE DISK SEAT RlNG I Seat Ring Centerline Plane of Symme Through Olsk The methodology for calculating the thrust required to open the MOVs under the pressure locking scemuio is based on the Reference 1 (Roark's) engineering handbook. This methodology is based in part on calculations developed by MPR Associates (Reference 2). The methodology determines the total force required to open the valve under a pressure locking scenario by calculating 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'omponent. These components are determined using the following steps. NUREG/CP4 152 3C-12

II II I

 ~
           ,
             ~

n

led as two plates attached at the center by a hub which is concentric with plane of symmetry is assumed between the valve disks.'This plane f symmetry is considered fixed in the analysis FIGURE 2 Hane of Symmetry Modeled As: -I Axis af Symmetry 3C-13 NUREG/CP-0152

                                                                ~ ~ IJQ    (~ l~ i ~ %4gt 44+      b.~Q  ~q~+     C gascxf on this geometry, the fo>>o~ing constants are calculated using the Reference   i equations:

Average DPAcross Disk P+ P~ OP~ Pbo Disk Stress Constants D- Ext (Reference I, Table 24) 12x/1- v'-

                                 .2x(1+ v)

Geometry Factors b (Q.g b's FM~INB (Reference 1, Table 24) C2 = 4 1 1+2 (4) b'2 C =4a b a

                                                  +1 a

b

b a 1 I CI =- 1 I+ v+(1- v) a 2 b 1+v a 1-v 1- b 2 C9 = (7)

a 2 b 4 a hHGKG/CP4 152 3C-14

gQ a(, ji L)- 4~

                                                               ++~eh ~pn+                            C V) qz c The pressure force is assumed to act uniformly upon the inner surface of the disk between the hub diameter and the outer disk diameter. The outer edge oi the disk is assumed to be unimpeded and allowed to deflect away from the pressure force.

In addition, the disk hub is 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. FIGURE 3 shear

                                                                                                          ~am.
                                                                                                    ~  stretch PuP2            P3 Addtdonal Gccwcny Facmrs
                                           ,1 (lbfcrcncc l. Toblc24)
                                                                           ]+(]+v)

(r, ~ b for'Cacc2L) Moment F~ () $ g~s g ('D()

                                              -DP     x        C  -

c i (()(2ssasaa 2 Ta(sla 24,Csaa2L) hf>> (a -as ) Lss] 2

                                            ~DPav    ~     ~)

(r, ~ b for Cocc2L) 22(b ( Dcjfccclccc jhraprccc()tel bcatbg a(s(a2( Ccaa2L) yk(a a'iCs Q(s - .D Cs DPassg a a'PalaasaaL1 (ss 3C-15 NUREG/CP4152

4 ~bc X~Wi-o~ A,LO.E- KC -O~ ~ 0 44 ~~4 ~a~% C C S ~+ ~~Co Deflect to from pressure.'hear (peference 1, Table 25, Case 2 L) Ksa = -0. 2t '-2l (13) K,. x DPavgxa'xG (r, = b for Case" L) Deflection Po pressure I hub stretch P> = tr (a' b') DPavg

                                                          -Pj           L n  xb'2xE Total Deflecti ondueto pressure (17)

An evenly distributed force is assumed to act between the valve seat and the outer edge of the valve disk TNs 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. Therefore, the deflection due to the known pressure load must be balanced by the deflection due to the unknown seat load. The deflection due to the pressure force was previously calculated. The Reference 1 equations are now usod to determine the contact force between the seat and disk which results in a deflection which is equal and opposite to the deflection due to the pressure force. This is done by first calculating the amount deflection created by a unit load of seat const force (w ~ 1 lbf/in). The equilibrium contact load is then determined by dividing the deflection caused by the unit contact load into the previously calculated deflection due to the pressure force. The equations are provided below. NUREG/CP %152 3C-16

i~a + o~ k<O >- 4>-<< ~ hA4. Ac% w ca+ p~gg Q Q o+ C-Z4 rfdditional Geometry Factors l a 2 (Reference I, Table 24, Case IL) L,= rn 4xa a ro

                                                                                   +I   I

r, r,

                                                                                               +  -I a

(18) (for Case IL, r, = a, . L3 = Q = 0) >>0 a I+ v 2 I a ro

I-v 4 -H Deflectionjom sea load /bending (r,=a) ~,~ pc/yp (Reference I, Table 24, Case IL, w = I) (2o) Deflection f>>om seat load/sltea>> (>> =a) (ReferenceI, TaMe25,CaseIL,w=1) E'-12 ' (21) a b y =E (22) Deflectt'onPomseat load Ihub cour. Zxg xa w= I, .'.'Cnryres.hefo>>ce=2xe xa y zxb (23)

                             '.=y Deflectionporn Total                                         uni seat load (w=1)                                                                    +y +y                                       (24) 3C-17                                NUREG/CP-0152

~ 0

g g4i~4 ~i>+ C C sa ~+'C~+ Therefore, the equilibrium contact nt t load'istribution (ibf/in) and the corresponding load applied to each seatt iss calculated. cu using the relationship bc}ow..

                                           , it'll eX. iscalculated fpp ~

Load per seat = 2 x g x a x (25'26

  'ri    'fi 'h Several methods may be uused to determine
                      '

this friction coc cient and e

',

an appropriate scat to disk friction coefficient. Using

an a force balance on the disk to,seat interface, thcc followin cq uation is derived for cal cu Iating e s tcm force required to overcome thc increased contact load between the seat and disk:

Fprcskek = 2xgrxax '[pxcos{8)-sin{8)jx2 (27) wlenil the lass 2 corraposdssothenumber of scam The static unseating force results from the oopenn pac king load and pullout force'due to wedging of the valve disk during closure. These loads are superimposed on the loads due to c pressure forces which occur during pressure locking. The value for this load is based on static test data for the MOVs. I~ The piston effect due to vaIve internal pressure acceding outside pressure is calculated using dard ln the standard 'usuy'equation usuy'eq This force assists movement of the valve stem in the open direction. F plsross cffecs = x D 2 srtlss x Pb<<<<, P<<III) 4 {2S NUREG/CPA 152 3C-l8

The reverse piston effect is the term used in this calculation to refer to the pressure force acting downward against the valve disk. This force is calculated as follows: (29) F,,= <xa x 2xP~ P,,P, xsing HGURE 4 P 1oanet P bonnet 3C-19 NUREG/CP-0152

                                          ~~ Xc     Io.+s'o<    EhtO  ~ t- h <0- << >

k44~~4 we~+ C

                                                                               ~   4K2c As mentioned previously, the total stem force (tension) required to overcome pressure lochng is the sum of the four components discussed above. All of the terms are positive with the exception of the piston effect component.

(30) DESCRIFMON OF TEST VALVES The three test valves were obtained from different sources. The Crane valve is a test valve located at Quad Cities Station. The Westinghouse valve was obtained through the Westinghouse Owners Group. The Borg-Warner valve was obtained from Arizona Public Service. The Cram valve is a spare valve which was subjected to blowdown testing at Wyle Laboratories in Huntsville, Ahlmmt. The Westinghouse valve is a test valve which was subjected to limited testing at South Texas Project. The Borg-Warner valve was a spare valve which had not been subjected to previous testing other than that performed at the vendor prior to delivery. Thc Crane valve is a carbon steel valve (Model 783-U) which was modified during blowdown testing to contain a stainless steel valve disk and malcolmized guide rail (similar to the Model 783-UL valve design). The Westinghouse valve and Borg-Warner'alve were stainless steel valve designs. NUREG/CP4152 3C-20

11

                                                  ~ Xc     ~~W~q>        K~@, (         Z xy-u gg4hc4 ~+~+

c 4 C DMM~'IONOF TEST'APPARATUS The figure belo w shows the basic test setup used for the pressure locking tests. A VQTES'4 t acquisition system and a Motor Power Monitor (MPM) data acquisition system were used to collect stem thrust, actuato r torque and motor power data. In addition, on-line pressure data was collected during the Westinghouse and Borg-Warner valve tests. A hydrostatic test pump and accumulator were used as the pressure source during pressure locking tests and hydrppump DP tests: HGURE S MPM VOTES system m Llmttarq. S>>In Ga" Qe Accumutator 88 Pressure Pressure Gauge Gauge Hydro Pump

                                                                                     ~1 Vent Vent Pressure                    Pressure Gauge                       Gauge For the Crane test, the valve was laid on its siCk with the stem slightly below horizontal. This configuration was used to enlire that no air pockets would be trapped within the valve body when it was filled with water.

The Westinghouse valve was installed in a test stand with the stem upright. The valve bonnet was vented by bleeding air out of thk packing leakwff line.

The Borg-Warner valve was installed in a special test stand which allowed pivoting the valve

      'erline abo ut 1'ts cen         The valve stem could be put at any angle between upright and sloped
                                                                       ~

downward at a 15 degree angle in either direction. To remove air from the valve bon bonnet, the

                                  ~  ~       ~    ~

valve was rotated on its siCk and rocked up and down as it filled with water. 3C-21 NUREG/CP4152

DESCRY'TION OF TEST METHODS The test process started with static test strokes to verify the proper installation of the data acquisiti systems and to measure static unseating load magnitude and repeatability. LLE K RAT T Local leak rate tests of the valves were performed to measure seat tightness. These tests wi performed at multiple torque switch settings in some cases. DP Tests in the open direction were performed by pressurizing the valve from one side with hydropump and then stroking the valve open. Test data indicates that the differential pressure i maintained across the valve disk while the disk slid across the valve seat. The purpose of the DP tc was to precondition the valve seats and disks and to monitor the seat-to-disk friction coefficient. DP tests were performed until a stable friction coefficient was achieved. A series of pressure locking tests was performed fot each valve. Inlet pressure, outlet pressure, bon pressure, and static seating force were varied during these tests. Static baseline tests to measure static unseating load were performed between the pressure locking tests. Thc closure strokes for static tests were performed at the same initial conditions (pressure and seating force) as the clos strokes prior to the pressure locking tests so that the change in unseating load due to pressure lock could be accurately determined. To measure the seat tightness, bonnet deprcssurization rate tests were performed. The entire v assembly (including the valve bonnet) was pressurized while in the closed position. Then the upstr and downstream pressute wcte vented. The bonnet pressure as a function of time was measured. To'easure thc potential for pressure locking due to bonnet fiuid heat-up, thermally induced boy pressurization rate tests were performed on the Westinghouse and Borg-Warner valves. After ven air from the valve bonnet cavity, each valve was closed while filled with water at approximately psig. The valve bonnet was then heated using an outside heat source. The pressure of the fluid in valve bonnet was measured directly. The temperature of fluid in the valve bonnet for the Borg-Wa valve and the temperature of the outside of the valve bonnet for the Westinghouse valve were measu Initial pressurization rates between 0.5 and 2.0 psi/degree F were measured. Much higher ultir NUREG/CP4152 3C-22

1 klO < Ab-o 9 C tW e 4C.~W pressurization rates were witnessed during the Borg-Warner tests. The data from this testing is not presented in this report, but is available from ComEd upon request. PRESSURE LOCKING TEST DATA The following table provides the pressure locking test results comparing the measured pressure locking unseating load to the predicted pressure locking unseating load: TABLE 1 ercent IncraLse Conservatism Notes (Non-Cons.) 1 4 1 14 fan4 1 4

                                                                                             ,4 el fg    o fg    o fg    o fg-                                                  1  4 fg    e fge   ~                                                                    el 4 fge   ~

fge ~ fge ~ fg ~ 3ce23 NUREG/CP-0152

6 +~~M ~Vw+ c.g( e% ( tattc c ercent Unseating lncratse d 'onservatism Notes Thrust Increase (Non-Cons.) fg o i 1 4 fg o I org- 1 4 rg- . IO rg- . I rg- . I rg" ~ I NOTES:

1. The percent conservatism values are calculated after a "memory effect" of 3100 lbf (at TSS=1) or 3500 Ibf (at TSS=2) is added to the predicted pressure locking load. Testing indicated that the process of applying and then relieving pressure against one side of the closed valve was sufficient to cause the unseating force to increase by these amounts, even when no pressure was captured in the valve bonnet. This effect was only noted for the Borg-Warner test valve.

2. When bonnet pressure significantly exceeds the pressure class rating of the test valve, the pressure locking calculation methodology appears to become non~nservative.

3. Tests 86 and 95 were performed to quantify the "memory effect" for the Borg-Warner valve.

Thcsc tests were performed like a pressure locking test in that high pressure (- 600 psig) was put against one side of the valve disk and then bled off. However, any pressure that entered the vaLve bonnet was relieved prior to the opening stroke. J

4. The AC motor for the test valve staned during this test and the valve did not fully unseat.

Test data suggests that open valve motion was initiated prior to thc stall. Consequently, the measured. increase due to pressure locking is believed to be. correct.

5. Thc pressure data for this test is questionable and is being evaluated at this time.

II

6. The upstream and downstream prcssure during these tests was approximately 350 psig. This was done to approximate, the LPCI and LPCS injection valve pressure conditions which could exist in the event of a LOCh.

Graphs 1 through 6 provide thc data in Table 1 for the three test valves. Thc total measured unseating load versus the total predicted unseating load and the pressure related portion of the measiued load versus the predicted pressure related portion of the unseating load are plotted for each valve. NUREG/CP%152 3C-24

IP

It

GRAPH 1 Predicted Unseating Thrust Versus Measured Pressure Locldng Unseating Force for Crane Valve 'I sxNO tm 1mo 0 0 10000 20000 30000 4XOO 60000 000 70000 80000 Total Predicted Uneealng Load 3C-25 NUREGICP-0152

GRAPH 2 Predicted Versus Measured Portion of Pressure Thrust bue to Pressure Forces for Crane Valve 4XNO 35000 30MO 25000 20000 15000 10000 5000 0 0 5000 10000 15000 20000 25000 30000 35000 4XNO Predicted Load Due to Pressure NUREG/CP-0152 3C-26

r, oow Ro) he%) cpu GRAPH 3 Predicted Unseating Thrust Versus Measured Pressure Locking Unseating Thrust for Westinghouse Valve'O 5000 C co 8000 'I g axo 1000 0 0 1000 2000 3000 4000 5000 Total Predicted Unseating Thrust 3C-27 NUREG/CP-'0152

GRAPH 4 Predicted Yersus Measured Portion of Unseating Thrust Due to Pressure Forces for Westinghouse Valve a 7000 8000 Ch 5000 g m <<xe ceo axe

           '1000 0    1000   2000     3000 4000 5000  6000 7000 Predicted Laad Due to Pressure NUREG/C F4152                      3C-28

I) GRAPH 5 Predicted Unseating Thrust Versus Measured Pressure Locking Unseating Thrust for Borg-Warner Valve 10000 15000 '0000 25000 Predicted Unseating Load 3C-29 NUREG/CP-0152

0 GRAPH 6 Predicted Versus Measured Portion of Unseating Thrust Due to Pressure Forces. for Borg-%amer Valve 10000 " 1$ 0 8NXS PrecHcted Pnasure Fonee NUREGICP-0152 3C-30

14 K~l~+ o ~~a.i- h b- Oo ~ P o 1 c.zw 4- c>4 PRIMARY DIN'ERENCES BETWEEN THE COMMONWEALTHEDISON PRESSURE LOCKING CALCULATION AND THE PRESSURE LOCKING CALCULATION METHOD PUBLISHED IN NUIT/CP-0146 The ComEd methodology is based on calculating the contact load at the edge of the disk which results in an equal and opposite disk deflection to that caused by pressure trapped between the disks, The ComEd methodology differs in several ways from the methodology described in the Reference 4 NUREG.

~ The NUTMEG Methodology ignores disk deflection due to hub elongation. This is non-conservative. For typical disk geometries, the expected impact of ignoring this effect is less than 5%.

~ The hKGKG Methodology is based on using Table 24 of Roark's equations for calculating forces in the disk. This table ignores disk deflection duc to transverse shear stresses. Section 10.3 of Roark's Equations discusses the conditions under which deflection due to shear is negligible. For typical disk geometries the deflection due to shear is often not negligible. Table 25 of Roark's Equations provides the equations for calculating disk deflection due to shear. Ignoring deflection duc to shear is non~nscrvativc. For small valve sizes where the disk thickness to disk diameter aspect ratio is large () 0.3), ignoring shear may result in under predicting the disk to seat contact load by 10% or more, The ComEd methodology treats the vertical pressure force on the disk separately from the pressure lochng load caused by the increased contact load between the seat and disk. The NUREG methodology relies on use of the open disk factor for translating the increased seating contact force into an increased unseating load. The open disk factor is based on a free body diagram in which the disk hub is unloaded. This is not the case for pressure locking. The NUREG treatment of these two components to the pressure locking unseating load is non-conservative. This source of nonmnservatism is generally much more significant than the other concerns mentioned above for the NUREG method and is the primary ComEd concern with the NUIT method. The derivations on the following pages are provided to support the discussion above. 3C-31 NUREG/CP-0152

Op~ phAT eACTOR DERIVATlON (Opening a valve against a differential pressure)

                                                                               %~%~4 o~ ~'

F = Stem Force (tension) pic i- ~u-'~+ p ~4 ~ p~i+C P = Pressure Force < g ~ q, c+ CZG FIGURE 6

DP x Seat Area R = Seat Reaction Force pR = Seat Friction Force 8 = Seat Angle Disk Factor (VF) = F / P (by definition) Sum of forces in direction: g F, Peos8 Rcos8 -@csin-8 (31) cM8 (32) P cos&+ psia& Sum of forces in y~ction: Z~~e.-h e iam- (33) coe& F Psfn& P . sh8-peas&} coe&+ csin& sh cps&+yah& sh&-icos&)

cos&+psh& cos&+psh8 F sin&coe&+psin&~&sh&+ col P (34) P coe&+psh8 hKHKG/CP4152 3C-32

4' fQ.'I. 5 c h, h.Q ca% Q.o

                                                                         +~ 4i          ~~%     C PRESSURE LOCKING SUM'OF FORCES                                          W~qq        C  >w Q.++ 4 F     = Stem Force (tension)

P = Pressure Force

                                                         = DP x Seat Area FIGURE 7 Q,   =  Seat Reaction Force (calculated using Roark's) p,Q,  = Seat Friction Force
                                                  , 8    = Seat Angle T = Disk Hub Tension
                                 <a Note that the sum of the forces in the    x~tion       is different than for the seat factor case due to the hub tension force T. Consequently, the Q, value is a typically a much lower portion of the P value under pressure lochng than it is for the seat factor calculation. (This is the benefit of using Roark's equations for calculating the seat load increase.) Therefore, the sum of the forces in the direction should be solved for directly from the free body diagram above, as follows:

P Pz F pQ,esS -Psbdl+Qp-in8 (35)

.F qJpcos8-Iin8)+Mn8 The first term in the equation above is the pressure locking load term in the ComEd methodology. The second term in the equation above is the F or reverse piston effect term ~

in the ComEd methodology. The ComEd method adds these two terms to the static unseating load and then subtracts the stem rejection load to get the predicted unseating load under pressure locking conditions Rather than use these equations, the NUREG method applies the open seat factor to the Q, value. Because of the relationship in equation 37 below, the NUREG method substantially under predicts the vertical pressure force portion of the required thrust. Qa < P cos8/ (cos8 +p sin8) (37) 3C-33 NVREG/CP4152

I C- K 4 4'0 < tg.~ b.) -oa 'W R,<t h.~~+ ~pm' xvr. REHaMNCES nqq C+< c4 C2 Young, W. C., 1989, Sixth Edition of Roark's Formulas for Stress and Strain, McGraw-Hill Inc. n

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. Electric Power Research Institute, Nuclear Maintenance Applications Center, 1990, Application Guide For Motor-Operated Valves in Nuclear Power Plants, EPRI/NMAC Report NP-6660-D, March.

4. Smith, D.E., 1994, "Calculation to Predict the Required Thrust to Open a Flexible Wedge Gate Valve Subjected to Pressure Locking", Proceedings of the Workshop on Gate Valve Pressure Locking and 7hennal Binding, NUREG/CP-0146, July 1995.

NUREG/CP4152 3C-34

gc +So~ 6 lQ he@-~4 ~y ~+ P~)w 6 l < W1 2, GATE VALVETYPE, GEOMETRY, AND ITS EFFECT ON OPEMNG AND CLOSING THRUSTS There are five different types of gate valves that cover most of the applications in nuclear power plants in the United States. The key features of these designs are shown in Figure 2.1. Variations in the most commonly used gate valves include solid, flexible, and split gates (Figure 2.1a). The two types of parallel expanding wedge gates shown in Figure 2.1b are also used, but their population is smaller. Parallel sliding gate valves shown in Figure 2.1c are relatively uncommon in the United States, but are widely used in European nuclear power plants. The advantages and disadvantages of various design features for these valves are discussed in detail in Reference [13] Flexible Wedge Solid Wedge Split Wedge Gate Gate Gate Figure 2.1a Conventional Solid Wedge, Hexible Wedge, and Split Wedge Gate Valves As shown in these figures, the designs vary significantly in gate geometries. Other important variations that affect performance are related to gate guide arrangements and their dimensions; clearances at critical locations between gate, guides, and seats; seat contact widths; and materials and surface finish in the disc guide sliding interfaces. Section 2 presents the gate thrust requirements for the above-described variations in gate geometries. This section also addresses the potential for disc tilting during mid-travel due to fluid forces across the disc. Disc tilting causes localized loading between the disc and the downstream seat, or between the disc and the guides. A preliminary analysis approach to determine the localized contact stresses is presented in this section to determine the loading severity based upon valve design and operating conditions.

0 Preliminary analyses of localized contact stresses between disc and seats as well as disc and guides used in typical wedge gate valve designs are presented in this section. The preliminary approach presented here needs further analytical refinement and empirical correlations to develop improved predictive models. Detailed derivations of the equations summarized in this section are included in Appendices A, B, and C. Stom Down-Upper stream Wodge Disc Upstream Lower Disc Wedge Body Stop Pad Seat Sogment Figuxe 2.1b Parallel Expanding Gate Valves Stem Disc Retalnlng Pine Seat Disc Carrier Preload Spring Figure 2.1c Parallel Sliding Gate Valve

/I (' 4 ~ Waken A tn.i-

                                                                                                     ~p~+         ~l Waqg 2, l. Stem Thrust for Solid, Flexible, and Split Wodge Gate Valves
                                            'I Even though there are differences in the performance of solid, flexible, and split wedge gate valves as related to their sensitivity, to external piping loads and thermal binding [13],

the equations for their stem thrust requirements based upon free body considerations are the same. Subsections 2.1.1 through 2.1.2 summarize the stem thrust requirements to I overcome only the differential pressure load across the disc. Subsections 2.1.3 and 2.1.4 give the stem wedging and unwedging thrust requirements to close and open the gate, respectively. The total stem thrust requirements to close and operi the gate are provided in Section 2.4, which include other components such as stem packing load, stem rejection Nn force (also referred to as blowout force or piston eff'ect force), and stem and gate weight.

 ~am C

2.1.1. Ciosinl, Stem Thrust to Ouereome Gate Di/7erenti al Pressure Ivor As shown in Section A.1.1 of Appendix A, the stem thrust at the gate to overcome the dgo diff'erential pressure during closing can be expressed as: F,= . F (Eq. 2.1) [cos6-@sine where Fs = stem load at gate, Ib Fp Fp = disc pressure load due to upstream/downstream differential pressure, lb hP x (effective seat area) Figuxe R2 coefficient of friction between gate and seat Gate Equilibrium Under 8= 1/2 of gate wedge angle, deg' hP Load During Closing The disc pressure load, Fp, is the product of hP and seat area based on effective disc sealing diameter as discussed further in Section 2.5. From Equation 2.1 the relationship between the commonly-used term disc factor (some-times called ualue factor) and coefficient of friction, p, can be derived: Disc Factor = (Eq. 2. la) cos 8- p sin 8 For'ypical wedge gate valves that use a total wedge angle of around 10 degrees (or 8 = 5') and a normal range of coefficients of friction, the difference between the disc factor and the coefficient of friction is practically negligible, as discussed in Section 3.1. The disc factor calculated in the closing direction can be as much as 5 percent higher than the coefficient of friction for typical values of 8 and p that are encountered in practice.

I'c 2.1.2. Opening Stem Thrust to Overcome Disc Differential Pressure As derived in Section A.l.2 of Appendix A, stem thrust during opening of a wedge disc against a differential pressure is given by: F = ~ F (Eq. 2.2) cos6+I sin6 From this one can derive the equivalence between the disc factor in the opening direction and the coefficient of friction: Disc Factor = (Eq. 2.2a) cos 6+ iL sin 6 Figure R3 The disc factor in the opening direction is slightly less Gate Equilibrium Under than the coefficient of friction for typical ranges of wedge dP Load During Opening angles and coefficients of friction (within 5 percent of the coefficient of friction), as discussed in Section 3.1. As stated earlier, the stem force calculated in Equation 2.1 or 2.2 is the force required to overcome the differential pressure resistance only. 2.1.3. Stem WedgingLoad -Closing The stem wedging load is related to the normal seat contact force, Fn, as shown in Section A.1.3 of Appendix A: F,=2(sin 6+ p cos6) F (Eq, 2.3) It should be noted that this equation applies to the case when there is no differen'tial pressure across the gate. When differential pressure is present, the stem force Fs in this equation is the net stem Figure 2A Gate Equilibrium under force after subtracting the differential pressure Wedging Load During Closing load. In some cases, the limit switch instead of the torque switch is used to stop the disc travel in the closing direction. Where acceptable from the shut-off standpoint, this approach can be used to reduce, and in some cases eliminate, the wedging load, F.

\ Q h %+-a.~(~F

> 1,4. Stem UnwedgingLoad - Opening
                                                                                 ~~~~ 8 ~ ~wbg Section A.l.4 of Appendix A shows that the unwedg-ing load to overcome the seat contact force, F, is given by:

F = 2 (lL cos 9- sin 9) F (Eq. 2.4) The seat contact force, F, that is to be overcome dur-Fn ing the opening cycle is developed by (1) wedging load from the previous closing cycle, including inertia overshoot, (2) external piping loads, or (3) differential thermal effects between the valve body and disc. Section 4 provides an analytical method-Figure 2$ ology to predict stem thrust due to inertia overshoot, Gate Equilibrium under and Section 5 discusses external pipe load and ther-Unwedging Load During Opening mal effects that may influence the normal load, Fn. 2.2. Stem Thrust for ParaM Expanding Gate Valves This Subsection 2.2 summarizes the stem thrust requirements for closing and opening directions for the two types of parallel expanding gate valves shown in Figure 2.1b. The same stem thrust equations apply to both types of parallel expanding gate valves shown in this figure. The typical wedge an'gle used in the through-conduit type is 15 degrees, and for the double-disc type is 25 degrees. It should be noted that for coefficient of friction of 0.4Z (= tan 25') or less, the 25-degree angle between the wedge surfaces (also referred to as back angles) provides a non-locking condition between the wedges. 2.2.1. Stem Thrust to Overcome Gate Differential Pressure - Closing and Opening As shown in Section A.2.1 of Appendix A, the following equation applies to both closing and openihg stem thrusts to overcome gate frictional force due to Fn hP load; Fy F -pF (Eq. 2,5) where p = coefficient of friction between seat and disc Closing Opening Fp disc pressure load due to Hguxe RS upstream/downstream Gate Equilibrium Under hP Load During differential pressure, lb Closing/Opening = hP x (effective seat area)

(l 4

('iQ.i- h w4-~~ ~~ ay oo~ l20 I 2.2.2. Stem 7Vedging Load - Closing The stem wedging load for a parallel expanding gate valve is shown in Section A.2.2 of Appendix A to be given by: sill 6+ p cos 6 Fs p+ (Eq. 2.6) cos6-p'sin 6 where coefficient of friction between seat and disc X coefficient of friction between wedge Fp faces 6 parallel gate total wedge angle, deg Fn normal force between gate and seat due to Figure 2.7 wedging, lbs Gate Equilibrium Under Wedging Load During Closing This, equation makes allowance'or the fact that the coefficients of friction at the seat-to-disc interface may be different than that at the wedge interface. Typically the seat faces have a finer surface finish and are overlaid with Stellite hard-facing, whereas the wedge faces have a rougher surface finish and are not hard-faced. Ifthe coefficient of friction at the seat faces and the wedge faces is assumed to be the same, p' p, and this equation reduces to sin'6 1-li +2gcos6 Fs= Fn (Eq. 2.6a) cos 6-csin 6 Equation 2.6a shows that the stem load is proportional to the seat contact force, Fn. 2.2.3: Stem UnwedgingLoad - Opening The stem unwedging load to overcome the seat contact force, Fn, for a parallel expanding gate valve is given by (reference Section A.2.3, Appendix A):

0

                                                                     *a~ kia.l-         a~i      a~S 2c'l
                                                                                      ~s~+

((p p'- 1) sin 8+ (g+ ll') cos 6 F (Eq. 2.7) cos8~p'sin 6 I'or p = p ', this equation reduces to: sin 6 p -1+2pcos6 F- Fn (Eq. 2.7a) cos6+psin6-Figure 2.8 Gate EquiHbrium Under Unwedging Load During Opening As discussed in Section 2.1.4, the seat contact force Fn to be overcome is determined by adding the wedging force from the previous closing cycle to the resultant force from external piping loads and differential thermal expansion loads between the body and disc. 4 2>. Stem Loads for Parallel Sliding Gate Valves - Closing and Opening Most parallel sliding gate valves are equipped with a preloading spring to maintain proper contact and provide a low pressure seal between the disc and seats. As shown in Appendix A, Section A.3.1, the required stem thrust to overcome dP and spring load friction can be expressed as: FI=2pF>>+pFp (Eq. 2.8) where F>> = disc spring load, lb F>= hP x (eFective seat area), lbs

                                                <s A
                  <n
                                                   ~F ~P Dawn  ~w paW              llP ~~ p4 Figure R9 Gate EquBibrium Under hP Load During Closing

E gl

.0

A>CO tao>sa> S><')>> >> >>>a: VCS a>uu S>u>>CO 5>OS>> t>o >Orb>OS> >rs Ons iment: Af, au unit tangential bending moment; Q. ~ unit shear force {force per unit of c'Ircumferencial length); E ~ modulus of elasticity (force

unit area: v s Poisson's ratio; y ~ temperature coefftcient of expansion {unit strain per degree); a ~ outer radius; b ~ inner radius for annular

   >te; t ~ plate thickness; r ~ radial location of quantity being evaluated; r, ~ radial location of unit line loading or start of a distributed load. F, ul FO and G> to f'>are the several functions of the radial location r. C> to Cs are plate constants dependent upon the ratio aib. L, to L>> are loading                                                                             O nstants dependent upon the ratio air,. When used as subscripts, r and t refer to radial and tangential directions, respectively. When used as osc             . a. b. and o refer to an evaluation of the quantity subscripted at the outer edge, inner edge, and the posinon ol'he loading or start of I'oading.

f'(lls

cn respectively. When used as a subscript, r refers to an evaluation of the quantity subscripted 'at the center of the plate. are asar>cia(ed with the several quantities in the following manner: Deflections v and vo are positive upward: slopes () 2nd 84 are positive eflectio>> l increases positively as r increases; moments /)f~ Ill>. >>ml If are positive when creating compression on the top surface; and the O cn sr force Q is p>sitive when acting upward on the inner edge of a given annular section <n 0 Bc>>di>>g s(recses can be found from the moments /Ifr and Afr by the expreani>>r> o = 6M/t2. The plate constant D = Etal)2{) r ). The singularity (>>> iction brackets ( ) indicate that the expression contained within the brackets must be equated to sero unless r any other brackets. Note that Qa, Q, M, and Mare reactions, not loads. They exist only when necessary edge restraints are provided.

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 =-'.[        -(-:)']                                                                                 n--,'[ -(-.')']
 =    '[(-')'- i+ li.,']                                                                            2, =  '[(-')'                   i+   is -']
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08 0.1909 0.1640 -0.0122 0.7 OANI0 0.0149 04 -4.006t i,sj,SI Sl <<>> a OW 2 - \
~ ~
1st JJ ba s praas>0) a t,fc O.I 04 OS 0.7 0.9 O. I 4 4444 44$ $ $ ca OA024 P.SI52 4.1274 04 OS OANOO f O.l 77 0.1$ 7$ OANST OANOO 0.7 08 Yabsa of ~ 0.0$ 4$ OANOO 0.0741 0.0146
, ' [$ ($ $ ")s -'- ~ + $ "(-")'($ - ~$ ")] O.l 0.7949 -0.0000 n$ OA5$ 5 IL$$ 2 7 tiVsfa 6 > 0) 04 08 Od IO I 0~ 08$ 5$
0.175$ 0.1216 0.0619 0.7 Vabsa of ~ 0.1$ 0$ OAI9$7 OAI~ If 4.0$ aj 4.0 I 57 04 ts a OAIO 4 f
<<>> a
( ~ ) ]b, '; la~6>0) 4I, 4j, 4b, 41 0.10 S tsfc O.l Oa [ o L 0.7 0.9 O. I OANOO 0.2$ $ 5 04517 OAIIW v.oa OJ OANOO OAN94 0.0941 0$ 0.042 6 0.0000 4AISTS O.ott9 0.7 Vabsa of << 0.0000 0.049$ 0.9 0.0040 0.1 08791 OA905 04407 O.f 472 0.0555 t OJ 08 OMTO 0.'I 554 O.ltst 0.0460
+(-")'(IS- Itb -")) firer.s>0) 0.7 OAN90 OAN5$ 0.0251 0.9 OAIS12 0.01 f9 -0.0021
(Enclosure 2 consists of the Disposition to Calculation No. A10.1-AD-003, titled "Pressure Locking Evaluation of MOVs." Enclosure 2 has 13 pages,
~ ~
which are numbered from 1 to 13)
0 T NAGARA Peoe 1 INaxi) V NUCLEAR MOHAWK ENGINEERING 0'tel Li(t't i 3 u Project: NINE MILE POINT NUCLEAR STATION Unit (1,2 or 0=Both): ~ Discipline: +<<~~ Ti le Calcullt tion No. Rev Disp m~f.c o s, Uac.'(I('eg l:- u Ku- I('o~ A,tOd'l- A5-OO~ 0 t g I P, Wo< s nginator o~r~>> 4 6 c-~a A,,q, ate M/r r Ag
/
(Sub) System(s)
~mP Index No. Checker Date Change No.
KePS+Cfir Approver V Xe+JOlO Ae~ "'- Date
/lrql /9 Safety Class: (SR/NSR/QXX): NMPC Acceptance/Date Superseded Document(s): Q,om(
Descnption of Change hwpeetA'aw iw ~(a'R~~ +o ~.~~~~"t ~~~'>" " + I ~ 'f4%. C,N'%(4 4 ~~~d'1 waif RI
'2 ~ P w ~on 5'7A/Q, ie %he. P~y'E~~
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4P th~ce.i4 pr~is~a,s.Cw %dasrt Id( ~ C
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~ +%~ ~ur.le 4 ~~4 I)~~>~~
C 4 W.hruS1' 5
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gg,'ro,.i( o> ua P Cross Reference Changels): tZ- eeW 97- 03 4 on irmaoon equire es o: ina ssue tatup i e ocation perations cceptance See Page(s): (APPIFIO/(/OII: + Pi (Ca(outa(/oo/Heidi:+d(d Rea d(Yea(I/'IAI: (d Cl Evaluation Number(s): 2 Og 3T 0 - 7 0%'h Component IDls)(As shown in MEL): Copy of Applicability Review Attached) Yes rU~ 29%9 fC A L-pP<<ops), Z5g+'o C Ã-V-4 2.~Ps ~gcgfge maw WnV O( a+A4 - 7 Key Words: F ~s~ P v Woe c 7n- +<T c '7A oo Thrc s(~ z~~ p ~ woo > 4 '7 . ArWg2 I g+ / r 9> <<O7 ws ~ p + WMM /b- D c
/3 AG7 I
((e f aa 0 r SOS f0 34 2l Page 25 NEP-DES-08 Rev 04
0 Niagara Mohawk Power Corporation NMP2 Page2ot Ato.t.AD%03, Rev. 01 t3 NuctearEngineering Calculation Cont. Sheet Originator/Date Dno~'mQ ~ 4 Q~ /cf /<~(>~ Checker/Date gVtt IJrq /R < Disp. 01A Valve ID no: ";"<<VP'"'IQVtGA Re uired 0 enin Force Deternmination under Pressure Lockin Conditions COMED Method DESIGN INPUTS: Design Basis Conditions at time of Pressure Locking Event: Upstream pressure (psig), P .'=108 Valve Bonnet pressure (psig), P bonn<<.=108 p pressure (psig), P down 0 'ownstream Valve Disk Geometry: I hubradius, b:=3.375 meanseatradius, a .'=3.91 averaae disk thickness, t:=0.48 6:= a n hub length, L:=0.125 seat angle, a '.= 10 ~ 6 = 0.087 2 180 Valve Disk Material Properties: 6 rs r','2!r <.'/s.'.:..:2gie ot modulus of elasticity, E '.=29400000 Poisson's Ratio, v .'=0.3 Other Valve Parameters: Valve Stem Diameter, D stern .'=1.625 Static Unseating Thrust F po 9232
¹ (reference: Test 25, 70/6/94)
Valve Factor VF:=0.65 r'/eference: N.":R-2'-Ot0) CALCULATIONS: cos<6> Coefficient of friction between disk and seat, sin(6) VF 1 It =0 686 t reference Prte, up+ down Average DPAcross Disk, DPavg Pbonnet- gives, DP av< =54
'I Disk Stiffnes Constants, D:= E\ nnd G:= E 12 I-v 2 III 2 (2+2I) which gives, D=2.97710 and G = 1.131 10 ~
Geometry Factors, C2'.=-I 4 I- b a 1+2 In a
b C3',= b 4a b
+1 a
In a b
+ I b
a 1 C8:=- 1+v+ 2 b a C9 '=- - In + I 2 whichgives, C2 =8.91910 C3 =3.96510 C 8 =0.911 C 9 =0.121 COMED PL Valve ID: 2SWP'MOV66A page 1 EvaitjationlNPswp66aaa.mcd
1t
~,
Niagara Mohawk Power Corporation NMP2 Page 3of t'tt Catctrlation Cont. Sheet Ato.t.AD4103, Rey, 111 Nuctear Engineering Originator/Date ~ ~ 1~a e A8 ~X fflt~t~7 Checker/Date
/dc'//e lfv Disp. 01A Additional Geometrt/Factors, rp '.=b 2 4 2 2 -5 2+ ln-rp L11 '= 1 64 1+4 a
0 a 0
-4 a
0 a a rp L17 1 4
1-1- v 1-4
'0
a 4 a 2
'0 '+(1+v) ln rp a
which gives, L 11 =1.378 10 and L 17 = 8.641.10 Moment Factors, M rb'.=- DPavg a C8 which gives, 2 C9 f 2ab (a -r0 ) L r7 Qb'a 2b
-r0)
M,b =-8.373 and Qb =31.18 Deflection from pressure/bending, 4 a' avg a ybq 'rb
~ =
D
'C2+Qb D
C3-D L11 which gives, y bq =-1.937 10 Deflection from pressure /shear, 2 sa'vg .2a Ksa'3 2'In a b 1+ rp a
' 2'I rp b
sq'G which gives, K sa =-0.012 and ysq 1796 10" Deflection from pressure /hub stretch, P force'L (2 b force(a ) DPavg y stretctt
'abb 2E which gives, P f = 661.191 and y stre<ctt =-3.928 10 COMED PL Valve ID: 2SWP'MOV66A page 2 EvaluationlNPswp66aaa.mcd
/ 0 Niagara Mohawk Power Corporation NMP2 Page4of i3 NuclearEnginee ring Calculahon Cont. Sheet Ato.t.AD403. Rev.01 Originatorloate 'D c ~>~>e Q ~ I ~t W ~ f Checkedoate yves
~ +ii'><iqrt Disp. 01A Total Deflection due to pressure, y q:=y bq+ y sq+ y stretch which gives, y q =-3.771 10 Additional Geometer Factors r .'=a
0'p 1+v ln + . 2 2 1-v 1- ro L3 '.= . 4a ro
+1 ln +
a ro 1 L9'= a p 2 a rp 4 a a ro a which gives, L3 =0 and L9=0 Deflection from seat load bending,I w .'=1 y.b .= asw C2 rpC9 C8 b L9 p b 3
+L3 whichgives, ybw =-L83S 10 Deflection from seat load/shear, rp rp Ksa .'=-1.2 a
In- b y '.= Ksa tG a which gives, Ksa =-0.177 y sw 1'272'10 I Deflection from seat load hub compression, L ycompr 'b
, -2na 2 E
which gives, y compr = Total Deflection from unit seat load, y w:=y bw+ysw+'ycompr which gives, y w =-3.122 10 Equilibrium contact load distribution, yq w equilibrium
'w which gives, equilibrium = 12.081 yq =296.797 Load per seat= 2 n a yw Pressure Locking Force, COMED PL Valve ID: 2SWP MOV66A page 3 EvaluationlNPswp66aaa.mcd
e Niagara Mohawk Power Corporation NMP2 Pages ot+ NuclearEngineering Originator/Date Q ~ <~~~ lL,. ~ g lrgtyq Catoutaoon Cont. Sheet Cheotterjoate gvg y/rg/gg AlO.t-AD403. Rev. 01 Disp. 01A pres lock:= 2na '(it~os(8)-sin(8)).2 Vq Yw whichgives, Fp,es lock=354.165 Piston Effect Force, Pu aun =0 n>>
"piston effect ' 'tem '( bonnet atm which gives, F piston effect 223.986 'Reverse Piston Effect'orce, I
F een , [n'.=e (2 FOonnet np Oownj] ein(8) which gives, F vert 452 088 Total Force Re uired to Overcome Pressure Lockin, F tot I:=F pres lock+ F po+ F vert- "pisto~effect which gives,, F total = 9.814267 10 . ACTUA TOFt CAPAGILlTYt Actuator Nodei /Slzet = 8MB-00-1$
&fotor Torque Output: '=
TQm 14.74 ft- Ibs Gear Ratio: OGR:=41.0 Application Factor: Af:=0.9 Pullout ENciencyt Eff:=0.4 Reduced Voltage: RV:= 0.8838 Torque Oufput: TQout:=TQmRV OGRAf Eff TQout = 169.939 ft- Ibs Stem Factor; Sf '= 0.016407 Tht ust Capat3llityt TQout THcap:=
~
THcap = 1.036 10 lbs Sf iVOTEr RV lS SQUARE /F ACTUATQR IS AC. ENHANCED PRESSURE LQCKtNG NETHQDQLOGK KEI:='.20 Thrust Margin:= THcap- F >~.KEI Thrust Margin =-1.419 10 lbs ARy aot
Conclusion:
Open Thrust t0ergin is negative, therefore this valve and actuator are-~44~ overcome the theoretical pressure torking conditions evaluated. COMED PL Valve ID: 2SWP'MOV66A page 4 EvaluationINPswp66aaa.mcd
0 Niagara Mohawk Power Corporation NMP2 Page tc2ot l3 Nuclear Engineering Originator/Date 422~>~y~ A ~ g tgg(q y Catculation Cont. Sheet Checker/Date af/r4/4o A10.1.AD403. Rev. 01 Disp. 01A
Valve ID no: 282t V!'MOVE:~A Re uired 0 enin Force Deternmination under Pressure Lockin Conditions COMED Method DESIGN INPIJTS: Design Basis Conditions at time of Pressure Locking Event: Upstream pressure (psig), P .'= 108 Valve Bonnet pressure (psig), P bonnet 108 p Downstream pressure (psig), P down 0 Valve Disk Geometry: hub radius, b:= 1.25 mean seat radius, a'.=1.88 averaae disk thickness, t:=0.626 a x
hub length, L:=0.25 seat angle, a '.=10 e:= e =0.087 2 180 Valve Disk Material Properties: e js hair 'I pk ij)oje tx modulus of elasticity, E:=29400000 Poisson's Ratio, v '.=0.3 Other Valve Parameters: Valve Stem Diameter, D stern .'=1.375 'tatic Unseating Thrust, F po'.=4056 (reference: Test ¹ 8, 5/17/98) Valve Factor VF.'= I ( je/erence: NER-Bk0$ 0 ) CALCULATIONS: cos(e) Coefficient of friction between disk and seat, It:= 0 1 VF sin(e) It =1091 t referee::eft3 up+ down Average DP Across Disk, avg 'onnet 2 gives, DP ayg 54 Disk Stiffnes Constants, Et nnd G:= E 12 1-v 2(1+v) which gives, Geometry Factors, D = 6.605 10 C 2.'=-1 4 I- b a and 1+2 In a, G = 1.131 10
b C3 '.= b
'4a b a +I In a b + I a
C 8 '.= 1+v+(I 2
- v) ~ b a
2 C 9:=- - In + I 2 which gives, C 2 = 0.049 C 3 = 5.093 10 C 8 =0.805 C 9 =0.241 COMED PL Valve ID: 2SWP'MOV67A page 1 EvaluationlNPswp67aaa.mcd
II, Niagara Mohawk Power Corporation NMP2 Page'7 ot At0.t-AD%03. Rev. IP 01 Nuctear Engineering leapCalcutation Cont. Sheet Originator/Date Q ~,~ ~ 4 ~/Vl y Checker/Date X4
'I u] el~~
Disp. 01A Add/'tionat Geometr3/ Factors,'p'.=b 2 4 2 2 I+4 4 2y In-
~
I fp rp rp fp 64 a a a a rp 4 2. I I-v P 0 I+(I+v) In a L17 4 4 a a rp whichgives, L11=4.48110 and L 17 =0.046 Moment Factors, M ~b '.=- DPavg cg which gives, a 2 C9 2ab l (a - r 0 ) - L ~r ob:= 2b
'"'(*- 0*)
M rb --13.186 and Qb 42.593 Deflection from pressure/bending, a a a avg ybq:=Mrb C2+Qb C3- L11 D D D which gives, yh =-1.752 10 Deflection from pressure /shear, 2
'.3 2 a
In 1+ rp 2
~
I 2 In-brp sa'vg a Ksa t.o b a which gives, K sa =-0.078 and ysq =-2.09 10 Deflection from pressure /hub stretch,
-P force L orce(al2 -b ) DPavg y stretch 'tb 2E which gives, P force 334 525 and y stretch =-2.897 10 COMED PL Valve ID: 2SWP'MOV67A page 2 EvaiuationlNPswp67aaa.mcd
ll 0 18 lp
Niagara Mohawk Power Corporation NMP2 Page ~ot t 3 Nuclear Engineering Catcutabon Cont. Sheet Ato.t.AD403. Rev. 0t Originaterlnate Qss~ lW~ g'~ /+ f< 0 IO) CheokerrDate gad N/err/W Disp. OtA Total Deflection due to pressure, yq '=y bq+ y sq+ y stretch hfch gives yq =-4.131 10 Additional Geometry Factors rp.'=a L3'.= rp 4a ro a 2
+1 ln + -1 a
ro ro a 2 L 9:= . a
ro I+v 2 ln + rp a I-v 1-4 a 0 2 which gives, L3 =0 and L9=0 I Deflection from seat load bending, we 1 y'bw awC2p9 D C8 b Lg rp C3 b
+L3, evhichgivss y bw =-1.465 10 Deflection from seat load shear, I fp rp Ksa .'=-1.2 a
ln- b y',= Ksa a tG which gives, Ksa =-0.49 y sw =-1.301 10 I Deflection from seat load hub compression, L
,'= -2na 2 which gives, 1 023 0 y compr compr 1 nb E Total Deflection from unit seat load, y w:=ybw+ysw+ycompr which gives, y w =-2.868 10 Equilibrium contact load distribution, w equilibrium 'hich yq yw giv w equilibrium 14'406 yq =170.165 Load per seat= 2 n a yw Pressure Locking Force, COMED PL Valve ID: 2SWP MOV67A page 3 EvaiuationlNPswp67aaa.mcd
tl NMP2 Page Iof 17 Niagara Mohawk Power Corporation At0.t-AD403. Rev. Ot Nuclear Engineering Calculation Cont. Sheet ortginatorroate % +>~ 'to A. ~/~(ry (yq checkerroate ~
/vJ e/~/~~
Disp. ptA Yq F pres Ioc k'.= 2tt a (It cos(e)-sin(e)) 2 which gives, F pres lock w Piston Effect Force, P:=0 aun
'(/ =
2 piston effecttem bonnet atm wl Ich gives, Fpistpn effect 160.368
'Reverse Piston Effect'orce, F vert '.a ~
2 P bonnet up gown sin(e) which gives, vert 04 Total Force Re uired to Overcome Pressure Lockin, F total:=F pres lock+ F pp+ F vert- F pistpn effec which gives, F to~ = 4.340478 10 ACTLrAWR CAPAGILITV'cfuetor IHodel /'ize: = SM8-000-5 Motor Torque Output: TQm ,'=5 ft- lbs Gear Ratio: OGR:=57.0 Application Factor: Af:=0.9 / Pullout Efficiency." Eff:=0.4 Reduced Voltage: RV l=0.8816 Torque Output: TQout:= TQm RV OGR Af Eff TQout = 79.743 ft- Ibs 8temF acfor: Sf:=0.014263 Thrust Capatv7ltrrr: THcap '.=TQout Sf THcap = 5.591 10 Ibs ItIOT'F; RtrIG SQUARE IF ACTLIATORIS AC. FWHAeCEO PRESSURE LOCIr,'AVO urETHOaoLOOI" KEI:= 1.20 Thrust Margin'.=THcaP- Ftot I KEI Thrust Margin = 382.299 lbs
Conclusion:
Open Thrust Nerain is Positive. fherefore this valve and actuator are Iilrely fo overcome the theoretical pressure locking conrIIBons evaluated. COMED PL Valve ID: 2SWP'MOV67A page 4 EvaluationlNPswp67aaa.mcd
Niagara Mohawk Power Corporation NMP2 PagelOol \g N trotear Engineering Catoulation Cont. Sheet At0.t.AD403. Rev. 01 ohginalorloate Q ~l~ j'e Ar ~/Vlcglp f checkerroate
+tIcrI Disp.otA re /r 9/Orr Valve ID no: BSSVP >;"Ot/6TB Re uired 0 enin Force Deternmination under Pressure Lockin Conditions COMED Method DESIGN INPUTS:
Design Basis Conditions at time of Pressure Locking Event: Upstream pressure (psig), P p.'= 10S Valve Bonnet pressure (psig), P bonn<< .'= 10S Downstream pressure (psig), P down 0 Valve Disk Geometry: hubradius, b:=1.25 meanseatradius, a .'=1.88 averaae disk thickness, t:=0.626 hub length, L:=0.25 seat angle, ct '.= 10 e:= a rt 2 180 e =0.087 Valve Disk Material Properties: e is h tir di:-'..;tngie a modulus of elasticity, E:=29400000 Poisson's Ratio, v '.=0.3 Other Valve Parameters: Valve Stem Diameter, Dstcm.'=1.375 Static Unseating Thrust, F~.'=2444 (reference: Test ¹ 13, 5/26/9B) Valve Factor VF .'= I I reference: NER-2'-Ot0) CALCULATIONS: cos(e) Coefficient of friction between disk and seat, p, .'= I VF sin(e) It =1.091 ("eference ="6; up+ down Average DP Across Disk, avg 'onnet 2 gives, DP avg =54 Disk Stiffnes Constants, Et and G:= E 12 I-v 2/1+ v) which gives, Geometry Factors, D =6.605 10 C 2'.=- I 4 I- b a
~
and I+2 In a, G =1.131 10 b C3.'=
'4a b
b a
+I ln a
b
+ I a
b CS:=- 2
'+'+('-') b a
C9 a
- '=-b I+v ln 2
a b
+
I-v 4 I b a which gives, C 2 =0.049 C3 =5.093 10 C 8 =0.805 C 9 =0.241 COMED PL Valve ID: 2SWP'MOV678 page 1 EvaluationlNPswp67baa.mcd
Niagara Mohawk Power Cofgoration NMP2 Pagetiof 1 2h Caioulation Cont Sheet A10.1.AO403, Rev. 01 Nooiear Engineering o 'creere roar af cr re A ~err(<+(rr ceeee rcce Disp.01A gute vb~)~o Additional Geometry'actors, rp:-"b 2 4 2 2 I 64 1~4 1'p a 5 rp fp a 4 a 2+ In-fp a rp L17 4 I I- I-
] y 4'
fp 4 fp a 2 I+(I+y) ln a t'p which gives, L11 =4481.10
'nd L 17 =0.046 Moment Factors, M fb:-"-
DP avg a C8 2
~ .C9 2'a'b a rp -L17 oh:= 2b '"'('- 0')
which gives, M rb "13.186 and Qb =42593 Deflection from pressureNending, 4 ybq:=Mrb D, a' C2+Qb D C3- avg D a L 11 which gives, y bq =-1.752 10 Deflection from pressure Ishear, 2 2 Km'DP avg K:=-0.3 sa ' 2 In Iy a I In-b rp ~ 2 fp ysq
'=
a which gives, K sa =-0.078 and ysq =-2.09 10 Deflection from pressure /hub stretch, ecerch 't force' b .2E which gives. p = 334.525 and y stretch = COMED PL Valve ID: 2SWP'MOV67B page 2 EvaluationlNPswp67baa.mcd
h I 0
Niagara Mohawk Power Corporation NMP2 Page 12ot 1 g Nuctear Engineering Cahuiation Cont. Sheet A10.1.AD403, Rev. 01 Ottgnator/DateWsem>>qual
~ (tt, gg9itrpy Checker/Date pe lr/ 19 /gQ Disp.ot A Total Deflection due to pressure, yq 'bq+ysq+ystretch which gives, y q =-4.131 10 Additional Geometry Factors .'=a rp -.
L 3 .'" 4a
'o a
2
+1 ln '+
a rp
'o -1 a
2 L9 '= . 1' a
1+v 2 ln a rp
+
1 4 v 1- rp a 2 which gives, L3 =0 and L9 =0 I Deflection from seat load bending, w .'=1 ybw.=- s w D C3 Cs
rccg -Lg b
.
r~C3 b s.L3 whichgives, y bw =-1.465 10 Deflection from seat load shear, I I ro ro Ksa .'=-1.2 a In- b ysw'sa a tG which gives, Ksa =-0.49 ysw =-1.301 10 Deflection from seat load /hub compression, L 2'tt 'a 2 y compr
'tb E which gives, cpm P r 1 023 10 Total Deflection from unit seat load, yw'bw+ysw+ycompr which gives, yw 2'868'10 Equilibrium contact load distribution, yq equilibrium 'w which gives, equilibrium Load per seat=
yq = 2 tt a 170.165 yw Pressure Locking Force, COMED PL Valve ID: 2SWP'MOV67B page 3 EvaluatlonlNPswp67baa.rncd
Niagara Mohawk Power Corporation NMP2 Pager 9of At0.t.AD403. Rev. 01 l3 Nuctear Engineering Calculation Cont. Sheet Ortgtnatorlnate Qep~~g > 4 ~4lj PbP Checker/Dale XV4 Vlr~l~z Disp.ot A F pres lock 2 rt a Yq W (p, cos(8 ) sin(0 ) ) 2 which gives, F pres lock = " Piston Effect Force, Pan:=0 effecttem 2 '(/p bonnet atm which gives, F piston effect = 160.368 piston
'Reverse Piston Effect'orce, F , I en'.=[n s (2 p bonnet np- psronss}] sin(8) which gives, F ert = 104.517 Total Force Re uired o Overcome Pressure Lockin, F total:= F pres lock+' po+ F vert- F piston effec which gives, F <<~ =2.728478 10 ACTUATOR CAPABILITYr Actuator Nodel Size: I = Sl'f8-000-5 '=5 ft- lbs Motor Torrfue Output; TQm Gear Ratio: OGR:=57.0 Application Factor: Af '=0.9 Pullout Efficiency: Eff:=0.4 Reduced Voltage: RV:= 0.8825 Torque Output; TQout:= TQm RV OGR AfEff TQout = 79.906 ft- Ibs Stern Factor: Sf:= 0.014263 Tlu ust CapBbflityr TQout THcap'.= THcap = 5.602 10 3
Ibs Sf NOTE: RV IS SQUARE IF ACTUATOR IS AC. ENHANCED PRESSURE LOC/C NG METHODOLOGY: , KEI:>> 1.20 Thrust Margin '=THcap- F to~ KEI Thrust Margin =2.328 10 lbs
Conclusion:
Open Thrust Margin ls posftivep therefore this valve and actuator are likely to overcome the theoretical pressure locking conditions evaluated. COMED PL Valve ID: 2SWP'MOV67B page 4 EvaluationlNPswp67baa.mcd
I 0 N 0}}

ML18040A362

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ML18040A362

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1.0 PURPOSE

2.0 SCOPE

3.0 METHODOLOGY

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