LR-N05-0446, ASME Code Relief Request Salem Units 1 and 2

ASME Code Relief Request Salem Units 1 and 2

ML053290158
Person / Time
Site:	Salem
Issue date:	11/16/2005
From:	Joyce T Public Service Enterprise Group
To:	Document Control Desk, Office of Nuclear Reactor Regulation
References
LR-N05-0446
Download: ML053290158 (66)

Text

PSEG Nuclear LLC P.O. Box 236, Hancocks Bridge, New Jersey 08038-0236 NOV NV1 66Nuclear 2005 0 SE LLC LR-N05-0446 U. S. Nuclear Regulatory Commission Document Control Desk Washington, DC 20555 ASME CODE RELIEF REQUEST SALEM GENERATING STATION - UNIT I AND UNIT 2 DOCKET NOS. 50-272 AND 50-311 FACILITY OPERATING LICENSE NOS. DPR-70 AND DPR-75 Pursuant to 10 CFR 50.55a(a)(3)i), PSEG Nuclear LLC (PSEG) requests relief from American Society of Mechanical Engineers (ASME) Section Vill, Division 1, UG-27.

This section does not permit the use of plastic analysis; however, ASME Section Vill, Division 2 does permit the use of plastic analysis provided minimum wall thickness requirements are satisfied and any seam welds are fully radiographed.

This relief request is being submitted in an effort to align the lower design pressure of the Component Cooling (CC) heat exchanger with that of the remainder of the Salem Service Water System. Analysis has been performed which demonstrates that there is adequate safety margin of the CC Heat Exchanger under the design pressure requirements. PSEG is requesting for deviation from the normal approach of performing calculations. The proposed alternative is to use plastic analysis of the CC heat exchanger using the methodology provided in ASME Code, Section Vil Division 2, 2004 Edition, Appendix 4, Paragraph 4-136.4.

If you have any questions please contact Mr. Justin Weame at 856-339-5081.

Sincerely, Thomas P. Jove Site Vice President Salem Generating Station Attachments (1) Relief Request SC-RR-W03.

95-2168 REV. 7/99

t Document Control Desk NOV 1 6 2005 LR-N05-0446 C: Mr. S. Collins, Administrator - Region I U. S. Nuclear Regulatory Commission 475 Allendale Road King of Prussia, PA 19406 Mr. S. Bailey, Licensing Project Manager - Salem U. S. Nuclear Regulatory Commission Mail Stop 08B1 Washington, DC 20555 USNRC Senior Resident Inspector - Salem (X24)

Mr. K. Tosch, Manager IV Bureau of Nuclear Engineering PO Box 415 Trenton, New Jersey 08625

Document Control Desk LR-N05-0446 Attachment 1 10 CFR 50.55a Request Number SC-RR-W03 Proposed Alternative In Accordance with 10 CFR 50.55a(a)(3)(i)

Alternative Provides Acceptable Level of Quality and Safety Component Description Component Cooling (CC) shell-and-tube heat exchangers (1CCE5, 2CCE5, 2CCE6)

Applicable ASME Code Edition and Addenda:

American Society of Mechanical Engineers Boiler and Pressure Vessel Code (ASME Code), Section VilI - Division 1, 1968 Edition, with No Addenda (Reference 1),

Paragraph UG-27 provides the requirements for the minimum wall thickness.

Reason for Request

Background The current design pressure for the tube-side (head) of the heat exchangers is less than the Service Water (SW) System design pressure. The vessel design pressure is 150 psig versus a SW system design pressure of 200 psig. The SW system typically operates at a pressure under 150 psig. However, under certain system cold weather configurations, the operating pressure can increase above 150 psig. The maximum operating pressure would occur following a loss-of-offsite power (LOOP) event due to the combination of three pumps operating and decreased winter flow demand as the Containment Fan Cooler Units (CFCUs) and non-safety flow loads are automatically isolated. In this configuration, the system pressure is expected to be approximately 180 psig, with some components experiencing slightly higher pressures due to hydrostatic pressure.

Inorder to address this issue, an evaluation was performed of the SW side of the heat exchangers to demonstrate that the ASME Code margins are maintained at the worst-case operating conditions. The goal was to demonstrate acceptability of the SW side of the heat exchangers to 200 psig for compatibility with the system design pressure. This analysis is documented in S-C-SW-MEE-1882 (Enclosure 1). The evaluation concluded that the CC shell-and-tube heat exchangers are acceptable per the original Code to 154 psig. This pressure was limited by the minimum wall thickness requirements of the Code for the channel (i.e., the channel head minimum wall thickness criteria per Paragraph UG-27 are not met for higher pressures).

Specific Code Issues This relief request is to permit the use of an alternative analysis that will demonstrate that the CC heat exchangers meet the intent of the ASME Code for a pressure of 191 psig. This pressure (191 psig) is high enough to satisfy all of the system pressure requirements for the CC heat exchanger.

1

Document Control Desk LR-N05-0446 Attachment 1 10 CFR 50.55a Request Number SC-RR-W03 Proposed Alternative In Accordance with 10 CFR 50.55a(a)(3)(i)

Alternative Provides Acceptable Level of Quality and Safety The standard ASME Code calculations identify three areas that do not meet the standard Code requirements at the higher SW pressure (191 psig). Specifically,

1. The existing channel head wall thickness is 0.625 inches versus a required wall thickness 0.756 inches.

2. The existing nozzle reinforcement area is 7.48 in2 versus a required reinforcement area of 14.17 in2.

3. The existing channel flange minimum thickness is 4.63 inches versus a required thickness of 5.05 inches, based on maintaining an allowable stress of 17.5 ksi.

Proposed Alternative and Basis for Use:

Proposed Alternative The proposed alternative is to allow the use of plastic analysis of the CC shell-and-tube heat exchanger channel using the methodology provided in ASME Code, Section Vill -

Division 2, 2004 Edition, Appendix 4, Paragraph 4-136.4.

Basis for Use The issues related to the channel heads were evaluated using a finite element analysis (FEA). The FEA (enclosure 2) evaluated the inlet/outlet head using a three-dimensional model, which included the head, the nozzle and the flange. This permitted a single model to address all three design code compliance issues, as detailed in the previous section. The FEA included both elastic analysis and plastic analysis.

A scoping elastic analysis, using the allowable stresses provided in Section Vil -

Division 1, concluded that the flanges and nozzle reinforcement are acceptable for a SW pressure of 191 psig. However, the additional support provided by the nozzles and the pass partition plate are not enough to limit the membrane stress in the channel head to less than the allowable stress. Hence, a plastic analysis was necessary to justify operation at higher pressures. Plastic analysis can support higher working pressures by accounting for such strengthening phenomenon as strain hardening, redundancies by load shedding to other locations and strengthening by changing the basic shape of the component (i.e., large deflections).

The original Code of Record (ASME Section VilI - Division 1) does not permit the use of plastic analysis. However, ASME Section Vill - Division 2 does permit the use of plastic analysis, provided the minimum wall thickness requirements are satisfied and any seam welds are fully radiographed. The CC shell-and-tube heat exchangers do not satisfy either of these conditions. The minimum wall thickness requirement is not met 2

r Document Control Desk LR-N05-0446 Attachment 1 10 CFR 50.55a Request Number SC-RR-W03 Proposed Altemative In Accordance with 10 CFR 50.55a(aX3)(i)

Alternative Provides Acceptable Level of Quality and Safety and the seam welds were only spot radiographed. Accordingly, the FEA results could not be used to support a formal Code evaluation of the heat exchangers. Regardless, plastic analysis was used to determine whether overall Code margins to failure (i.e., 2/3 factor of safety to plastic collapse) would be maintained.

The plastic analysis showed that the 2/3 factor of safety on plastic collapse was maintained for channel head elements subjected to internal pressure of at least 191 psig (even though the minimum wall thickness requirements are not satisfied). This was accomplished by accounting for such strengthening phenomenon as strain hardening, redundancies by load shedding and changing the basic shape of the component (i.e., large deflections). The head shell material is a 90-10 Cu-Ni material which is very ductile at 30% elongation. The flange is also constructed of a ductile material (carbon steel). The analysis approach is an adaptation of the Section Vil -

Division 2 procedure.

• A 15% reduction of the stress-strain curve was made to philosophically account for the joint efficiency associated with spot radiography. This is not in accordance with the Code, but was done to maintain the overall Code approach of penalizing allowable stresses based on the level of inspections performed.

• Allowable stresses were based on Section Vil - Division 1 allowable stresses.

When plastic analysis is used, the Code also requires that fatigue and ratcheting be specifically considered, because of the potential for higher than typical strains. For fatigue, the number of pressure cycles experienced by the channel heads is very low and the fatigue is not considered significant. Ratcheting is not considered a concern because the plastic analysis included a 15% reduction factor on the yield strength to account for the joint efficiency. This reduction is analytical, but in reality, sections will not develop plastic hinges until the actual minimum yield strength is reached, which is at higher pressures. Therefore, ratcheting is not considered to occur.

Conclusion Through the use of plastic analysis, it is demonstrated that the flanges and nozzle reinforcement are acceptable at a pressure of 191 psig, and that the inherent Code 2/3 margin to plastic collapse of the channel head (inherent in the ASME Code) is met for at least 191 psig. Based on this result, it is concluded that the heat exchanger provides margin that is consistent with the intent of the Original Code.

3

Document Control Desk LR-N05-0446 Attachment I 10 CFR 50.55a Request Number SC-RR-W03 Proposed Alternative In Accordance with 10 CFR 50.55a(a)(3)(i)

Alternative Provides Acceptable Level of Quality and Safety Duration of Proposed Alternative The proposed "one-time-only" relief request alternative is requested on a permanent basis for Salem Units I and 2.

Precedents None

References:

1. ASME Code Section Vil - Division 1,1968 Edition with No Addenda.

2. ASME Code, Section Vil - Division 2, 2004 Edition, Appendix 4, Paragraph 4-136.4.

Enclosures:

1. S-C-SW-MEE-1 882, Salem SW Heat Exchangers-Suitability for Operation at Higher Pressures, Revision: 0, dated 1/27/05, Attachment C, MPR Calculation 0108-0309-jlh-1, "Component Cooling Shell and Tube Heat Exchanger Service Water Pressure Rerate Evaluation - 1CCE5, 2CCE5 &2CCE6," Revision 0.

2. S-C-SW-MEE-1 882, Salem SW Heat Exchangers-Suitability for Operation at Higher Pressures, Revision: 0, dated 1/27/05, Attachment D, MPR Calculation 0108-0.309-jem-1, 'Component Cooling Water Shell and Tube Heat Exchanger Channel Analysis," Revision 0.

4

r Document Control Desk LR-N05-0446 Attachment 1 10 CFR 50.55a Request Number SC-RR-W03 Proposed Alternative In Accordance with 10 CFR 50.55a(a)(3)(i)

Alternative Provides Acceptable Level of Quality and Safety Enclosure I S-C-SW-MEE-1 882, Salem SW Heat Exchangers - Suitability for Operation at Higher Pressures, Revision 0, Attachment C, MPR Calculation 0108-0309jlh-1, "Component Cooling Shell and Tube Heat Exchanger Service Water Pressure Rerate Evaluation - ICCE5, 2CCE5 & 2CCE6," Revision 0, dated 1/27/05.

r Document Control Desk LR-N05-0446 Attachment I 10 CFR 50.55a Request Number SC-RR-W03 Proposed Alternative In Accordance with 10 CFR 50.55a(a)(3)(i)

Alternative Provides Acceptable Level of Quality and Safety Enclosure 2 S-C-SW-MEE-1 882, Salem SW Heat Exchangers - Suitability for Operation at Higher Pressures, Revision: 0, Attachment D, MPR Calculation 0108-0.309-jem-1, "Component Cooling Water Shell and Tube Heat Exchanger ChannelAnalysis,"Revision dated 1/27/050.

USER RESPONSIBLE FOR VERIFYING REVISION, STATUS AND CHANGES PRINTED '20051108 5-gGSW-MEE-1882 r p) 0 Page C-1 of C-38 Rh n-or Attachment C: MPR Calculation 0108-0309jlh-1, "Component Cooling Shell and Tube Heat Exchanger Service Water Pressure Rerate Evaluation-ICCE5, 2CCE5, &2CCE6" Revision 0

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• AMPR 320 King Street Alexandria, VA 22314 CALCULATION TITLE PAGE Client Public Service Electric and Gas Page I of 37 Project Task No.

Salem SW HX Re-rate 0108-0418-0309-00

Title:

Calculation No.

Component Cooling Shell and Tube Heat Exchanger Service Water Pressure Rerate Evaluation-ICCES, 2CCE5, & 2CCE6 0108-0309jlh-1 Preparer I Date Checker I Date Reviewer &Approver / Date Rev. No.

J. L. Hibbard R. Parkerson R. B. Keating 0 QUALITY ASSURANCE DOCUMENT This document has been prepared, checked, and reviewed/approved in accordance with the Quality Assurance requirements of IOCFR50 Appendix B. as specified in the MPR Quality Assurance Manual.

MPR.OA FormOAtal-l. Rev. I

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320 King Street Alexandna, VA 22314 RECORD OF REVISIONS Calculation No. Prepared By ked Ey Page: 2 0108-0309-jlh-i j1 Revision Alfected Pages Description 0 All Initial Issue.

Note: The revision numberfoundon each individualpage of the calculation canres the revision level of the calcuatlon In effect at the time that page was last revised.

MPR OA FonrOA-3. 1, Rev. 0

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320 King Street Alexandria, VA 22314 Calculation No. Prepared By Chyqed By Page: 3 0108-309-jlib-I 5 > g t- °J Revision: 0 Table of Contents 1.0 Purpose ....... 4 2.0 Summary.....*1* . .... . 4 3.0 CalculationBases ...... . ... 6 4.0 Calculation...... . ... ** . - . ...... .......... 7 4.1 Data . . 7 4.2 Mnimum Thickness of Cylindrical Shell 1...4.

4.3 Flange Bolt Tensile Area .. 16 4.4 Channel Flange Evaluation ................................. . 19 4.5 Manway Flange Evaluation .. 22 4.6 inlet and Outlet Nozzle Flange Evaluation. 23 4.7 Minimum Thickness of Flat Cover .. 24 4.8 Reinforcement Area .. 26 4.9 Tubesheet .. 30 4.10 Scismic Evaluation .. 36 s.a R te fe re n c ........................

es........................... 37 MPR OA Form: OA-3.1-3. Rev. 0 MPR QA Fen QA.3.1-2.

Farm: OA 3.1-2, Rev. 0 Rev. O UIPR OA Form: OA-3.1-3, Rev. o

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]

UreMP Rr Calculation No.:

M F Prepared By: 0108-0309-Jlh-1 MPR Associates, inc. Revision No.: 0 320 King Street AlexandriaVA22314 Cecked f Page No.: 4 1.0 PURPOSE This calculation is a Section Vm11, Division 1, 1968 Edition (Reference 1)evaluation of the Salem Unit I Component Cooling (CC) Heat Exchanger Nos. 11, 21, and 22. The allowable stress for the cover bolting is from the 2001 edition of the ASME Code. TMe heat exchangers are evaluated for an incrcase in the tube side design pressure from 150 psig to 191 psig. Only the heat exchanger components that are affected by the design pressure increase are evaluated. As such, this is a partial code evaluation of the tube-side of the Component Cooling Heat Exchangers and is an addenda to the original code evaluation.

2.0

SUMMARY

Results of the code evaluation for the Component Cooling Heat Exchanger tube-side pressure increase are provided below.

Pressure Part Wall Thickness

• Location" Require? 'Actual 'Resuft N 'Thickness' 'ickness'

,P in.* 710t

'Tube 0.013 0.035 'OkA

'ChanndA & B" 0.756 0.625 "Not OkA Tintet & out.Nozzle' 0.232 0.625 *Ok' TI 'Manway Nozza 0.263 0.313 "0k"

'Chandnllange" 5.035 4.625 "NotOka

'Manway Flange' 1.437 2 'OkW "ChannelA&BCover' 3.991 6.188 'Ok' "Manvay Covell 1.188 1.5 'okw

'Tubsheet" 1.966 1.5 'Ok' Flange Dolt Tensile Stress Area

!Location' "Required 'Actua' 'Result'

-Boft Area' BoltAreaw so n- ^i ba 2* PL7 " d CannelA& B" 30.1 30.2 'Ok-oMamsw5 S.4 166 'Ok'

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1. ( F r[' -- -

Calculation No.:

XM r Prepared By: "-: 01080309ilh-1 MPR Associates, Inc. Revision No.: 0 320 ingA Street CP Alexanrira VA 22314 Chce By:. R.*;td1r Page No.: 5 Inlet & Outlet Nozzle Flange

, "aLocation* *Design "Rating" T5 =

1'Inlet & Outlet Nozzle Flange" 240 191 Reinforcement Area at Nozzles f Locadon' 'Require" "Actual" P.e~szalt"

77. - 71L 2"I 'in. ^ 2- O""

Inlct/Oudet Nozzle" 14.17 7.48 "Mannvay 35.92 39.63 "Ok" )

Seismic Evaluation An evaluation of the pressure retaining components for seismic acceleration concludes that the stresses from seismic acccleration are negligible.

USER RESPONSIBLE FOR VERIFYING REVISION, STATUS AND CHANGES PP3NTED 005 1108 S-5-CSW-sIIEE-1882 0gej 0 Page C-7 of C-38 Ad Calculation No.:

WIM PR Prepared By: G 0108-0309-jlh-1 MPR Associates. Inc. Revision No.: 0 320 King Street Alexandria VA 22314 Checked By: A. ,

Pe P

No.: 6

]

3.0 CALCULATION BASES I. The joint efficiency for the tube is = 0.6 . This assumes the tube is a single sided butt weld and that no inspection was performed, which is conservative.

2. Joint efficiencies for the inlet nozzle and outlet nozzle are E = 0.8 . This conservatively assumes the weld is a single sided butt weld with spot radiography (spot radiography is specified on Reference 4).

3. The manway gasket is a full face gasket design. For the gasket seating load calculation, the gasket is assumed to have an OD equal to the bolt circle diameter minus the bolt hole diameter. This gives a smaller than actual gasket surface area, which is considered to give a reasonable load for the gasket seating load calculation.

4. The gasket area for the gasket seating load calculation is based on the gasket OD and ID; the area for the gasket seal to the pass partition plate is not included in the gasket area.

5. No credit is taken for the thickness of the 90-10 CuNi integral clad on the carbon steel manway cover and tubesheet.

6. The channel flange is evaluated as a loose type flange, i.e., no credit is taken for stiffening provided by the channel hub. This is a conservative approach that simplifies the analysis, since the flange ring and hub are different materials (carbon steel and 90-10 CuNi).

7. The manway flange thickness is evaluated with the approach in Reference 1. Paragraph UA-6(b)(2). Thbis provides the required flange thickness for a spherically dished cover with a full face gasket. This evaluation approach is suggested in Reference 1, Paragraph UA-56, since the typical flange evaluation in Appendix A is not applicable to full face gaskets.

8. The corrosion allowance of the 9010 CuNi materials is 0 inches based on Reference 13. A corrosion allowance of 0 inches was also used for the titanium tube.

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,r-XSW-MEE-1882g I.41.1.) '9 Page C-8 of C-38 P r B: Calculation No.:

LLUED Prepared By: ,: O108-0309-Jlh-1 MPR Associates, Inc. e n 320 King Street z Revision No.: 0 AWandria VA 22314 Checked By: eW, mzve xi Page No.: 7 4.0 CALCULATION 4.1 Data Design Conditions P.

• 19 -psi Tube-side design pressure PS 150-psi Shellide design pressure; Ref. 2, Data Sheet T, 200.F Tube-side design temperature: Ref. 2. Data Sheet Operating Conditions Ta~g.jaii E (90 + 99.3)-& F .2 Taw sgalt - 94.65F Average salt water temperature; Ret. 2, Data Sheet Tayw.ns E(113 + *OO).F + 2 T....., 106.5 F Average service water temperature; Ref. 2, Data Sheet Tan.f a (Tavjsalt + Tavgs+v) 2 Tag.t= 100.57F Average tube water temperature I-. ,

USER RESPONSIBLE FOR VERIFYING REVISION, STATUS AND CHANGES PRINTED '20051108 5-}C SW-MEE-1882 II-'. 3 ) 0 Page 0-9 of C-38 YQT;0- -o rAIM PR MPR Associates, Inc.

Prepared By: Ž c

Calculation No.:

0108-0309-jlh-1 Revision No.: 0 320 King Street C 6.t Alexandria VA 22314 Checked By: ,

1, 'e5 J Page No.: 8 Materials Component Material Reference Tube Titanium, Gr. 2 No. 2, Data Sheet Channel A & B SB- 71 90D10 CuNi No. 2, Data Sheet Channel A & B Cover SA-105, Gr. II with a No. 2, Data Sheet 90-10 CuNi Liner Channel A & B Flange SA-105, Gr. 11 No. 4, Grid D-2 Channel A & B Bolting SA-193, Gr. B7 No. 4. Grid D-2 Inlet & Outlet Nozzle SB- 171 90-10 CuNi No. 4. Grid C-2 Inlet & Outlet Nozzle Flange SA-181, Gr. 11 No. 4, Grid C-2 Manway Cylinder SB-171 90-10 CuNi No._5, p. 3 Manway Cover SA-516, Gr. 70 No. 5, p. 3 Manway Flange SA-516, Gr. 70 No. 5, p. 3 Manway Flange Bolting SA-193, Gr. B7 No. 5, p. 4 Tubesheet SA-515, Gr. 70 with a 70-30 CuNi Liner No. 2, Data Sheet Shell SA-515, Gr. 70 No. 4, Grid D-2 Nozzle Reinforcement Pad SA-515, Gr. 70 No. 4, Grid C-1 Cover Gasket 1/B" thick, MONEL jacketed Asbestos No. 5. p. 4 Manway Gasket 1/8 thick, Garlock 3400 No. 5. p. 5 I

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Prepared By:. i Ca!culation No.:

0108-0309-j.h-t Revision No.: 0 320 Kng Street C * (2014 Alexandria VA 22314 CekdB: Page No.: 9 Data for the Tubes, Channels, Inlet/Outlet Nozzles, and thc Manway Cylinder Actual wanl thickness 0.035

-tube; Ref. 2, Data Sheet and Ref. 3. Table 9.2-3 0.625 'ChannelA & B4 -Channels A & B; Reference 4, Grid C-7 1, -Inletlout. (N1iN2); Reference 4, Grid C-2 a0.625

-Manway, Reference 5, p. 5

,5 . 16) "Manway Nozzle" 4 od a 0.75 66.25 2

t.20 In

{ "ChanndA "Tu1be"

'Inle"d & OUL Nozzle 0r

' Outside diameter

-tube; Ref. 2, Data Sheet

-Channels A & B; Reference 4, Grid C-7

-Inlet/out. (N1/N2); Reference 4, Grid C-2

-Manway; Reference 5. p. 5

,1&625) "Manway Nozzle' id a ad - 2.t

( 0.68 "Tube idinI 1651 un 1, "ChannelA&B" Inside diameter 1,18 ) "Manway Nozzle ri; Id+ 2

( 0.34) "Tube" 325an 'ChannclA &B" Inside radius r, - 9.375 its It 9 wManway Nozzle"

'8.4" "Tube' Allowable stress at design temperature "ChanneIA&B -tube; Ref. 1, Table UNF-23; assume welded tube S. IIksl -Channels A & B; Reference 1, Table UNF-23 19.81 -Inlet/out.; Reference 1, Table UNF-23

!,9.s) 'ManV Nozzle -Manway; Reference 5, p. 3 r Tube" Joint efficiency lO.6 ) -tube; Section 32 "ChonaclA& B" En I -Channels A&B; Ref. 13 10.801 11 = "hnet &Out. Nozze -Inlet/out.; Reference 4. Grid B-2 1 0.7) *Manway Nozzle" ) -Manway; Reference 5, p. B

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M M PR Prepared By , > 0108-0309-Jlh-I MPR Associates, Inc. RevisionNo.: 0 320 lxrJrlngaYA Chedked By, PageNo.: tO IAlexandria VA 22314 Chce Ry Pg o:1 Gaskets ods (67875) 12(ChannzdA & Bin Gasket effective OD

-Channels A & 6; Reference 2, Dwg. No. G-15763 21.5 *Manway, Ref. 5, p. 5; assumed to be bc minus bolt hole diameter 12 .(-ChanndA & Jr) Gasket vwidth 0.57 -Channels A & B; Reference 2, Dwg. No. G-15763 (Olin -Manway; Ref. 5, p. 5; based on radial distance from od, to gasket ID d a odS - NS d = (6Z3) in -. ChnnelA & B) Mean gasket dameter Thickness of channel gasket; 7Ts, 8 1, Reference 2, Dwg. No. G-15763 li=(ChannetA &Bj Gasket factor

-Channels A & B; Ref. 5, p. 6 (6.6) -Manway; Ref. 5, p. 5 and Ref. 6, p. 35 3(M")-s Gasket seating stress (7'ChanirA& B" -Channels A & B; Ref. 5, p. 6 y: M3000) (21 'Marnway ) -Manway; Ref. 5. p. 5 and Ref. 6, p. 35 Filange Bolting Number of bolts (24 12 .(ChcnnetA & SH) -Channels A & B; Ref. 4, Grid A-2

-Manway, Re. 5. p. 5 (0.419 2 12 ("ChanneIA &B' ) Bolt area at thread root diameter

-Reference 7, Table 8.2.2 for bolt area A0693J -Channels A &B; Ref. 5, p. 5

-Manway; Ref. 5, p. 5 12.("CIWanWA & r' Allowable bolt stress at design temperature Sb a- . Reference 14 Table 3 25 WallsuMyi Sa z Sb Allowable bolt stress at room temperature Reference 14, Table 3

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R Prepared By: 50108-0309-jlh-1 MPR Associates. Inc. y RevisionNo.: 0 320 King Street Ch k.6 @ f ~

Alexandria VA 22314 eckedBy: , Page No.: 11 l langes 12= ( &B )

eChannA OD of flange A 71.125). -Channels A & B; Reference 4, Grid A 3 (625 -Manway; Reference 5. p. 5

-Md~anivW B=(66..25 ) b ID of flange based on pipe OD (see Ref. 1. Figure B-I Ii UA-448a))

)&625 lcd I Thickness of flange (4.6zs5 12.(YhannelA & ir ) -Channels A &B; Reference 4, Grid A-3

1. 2 ) Manwvayf -Manway; Ref. 5. p. 6 (not including clad)

Bolt circle diameter bc(E22 C22.75) 69.25-t 12= (wChanneMA & B)

. 'Manwqy )

-Channels A &B; Reference 4. Grid A-3

-Manway; Ref. 5. p. 5 Width of raised face on channel flange; wg 211 Reference 4, Grid A-3 Allowable stress for flange at design temperature Sf (1%)Uk; 12= (Chnne)A & Jr ) -Channels A & B; Reference 1, Table UCS-23

' Manwaf *Manway. Reference 1, Table UCS-23 Pl50.aj0w:- 240-p-u Allowable pressure for a 150.1 class flange at the design temperature; Ref. 8. Table 2 nlat Plates 12- uChaneA& Bn ) Flat head Wckness (not Including clad)

Ifl.1 a (6 LS1 Lss *i.n -Channels A &B; Reference 4, Grid D-8 "MarnwW

-Manway; Reference 5. p. 5 12.(ChannelA & B" Factor

-Channels A & B; Reference 1. Figure UG-340)

(0.25) 82' Monmy Manway; Reference 1, Figure UG-34(p)

Silo1' ) Allowable stress for plate at design bmperature 12(ChmelAl & B')<

Sfl. 5) a, -Channels A &E; Reference 1. Table UCS-23 2 Manvay ) -Manway. Reference 1. Table UCS-23

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- -i

.5-0-SW-MEE-1882  ?\ r) , Page C-13 of C-38 I . rLA A 1 fzft P - r<

Calculation No.:

MP -A Prepared By: L 01084309jlh-1 MPR Associates, Inc. RevisbnNo.: 0 320 King Street Reeviion Alexandria VA 22314 Checked By: k Page No.: 12 Tubes N, a 3400 Number of tubes; Ref. 2. Data Sheet pt Ia-i Tube pitch; Ref. 2, Data Sheet

-k Mean coefficient of thermal expansion for tube at in-F 100F (approximate average tube temperature);

Ref. 11, Table TE-5 Modulus of elasticity for tube at 10OF (approximate (200) (s ) 6 average tube temperature); Ref. I 1,Table TUI-5 Et = 1S.38x psi Shell id, a 65-in Shell ID; Ref. 2, Data Sheet

'jSa.Sin Shell wall thickness; Ref. 2, Data Sheet od, a Id$+ 2-t, ods = 66 in Shell OD La 25-ft + 1.75-in - 2.3.625Sin Length between tubesheets; Ref. 10, Grid D-6 L - 304.50 in Mean coefficient of thermal expansion for shell at

'.s5.73-10 "

• F 100°F (approxirate average shell temperature);

Ref. 11. Table TE-1, Material Group B Modulus of elasticity for shell at 100IF (approximate EJu linic'(200 2a8) average shell temperature): Ref. 11, Table TM-1, CcO.3%

EJ - 29.34 x JOpsi

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ree By Calculation No.:

FAR M P R Prepared By: I "- ~0108-0309-11h-1 1APR Associates, Inc. ,,, Revision No.: 0 320 lKng Street ChecleAOy eR. e J P-agaN.:1 PageNo.: 13 Alexandria VA 22314 CheckedBy.

Tubesheet itt E 3.5 n Tubesheet thickness, not including clad; Ref. 10, Grid C-6 Allowable stress for tubesheet at design S,5 1i7.5Asi temperature; Reference 1,Table UCS-23 Modulus of elasticity for tubesheat at 100@F I (2 5) od 0 1 (approximate average temperature); Ref. 11, Table ls =29.4 x. 108ps e ). TM-1, C<0.3%; the tubesheet material specification for carbon Is in the range of 0.3%; for this El, =29.34 xO1Ppsi calculation, it is conservative to use the modulus for carbon cO.3% (based on a trial and error approach)

Inlettoutlet Nozzle Reinforcement Pad S5 Inlet and outlet nozzle reinforcement pad thickness; Ref. 4, Grid C-1 04pad bt Inlet and outlet nozzle reinforcement pad OD; Ref.

4. Grid C-1 Seismic Qr a L5.g Seismic static horizontal and vertical acceleration; Ref. 9, Attachment B, p. B-3 ah r 1.2-Peq*ch :416-psi

Channel equivalent pressure for seisnic acceleration; Ref. 5, Paragraph 7.B.1 Feq.rn :- S40.bf Manway equivalent load for seismic acceleration; Ref. 5, Paragraph 7.B.2

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Calculatbon No.:

FAR zMP Prepared By:  % 0108.030911h1 MPR Associates, Inc. ,j' Revision No.: 0 320 Kng Street AlexandriaVA22314 C:hecked y: ,, PageNo.: 14 4.2 Minimum Thickness of Cylindrical Shell Determine the minimum required wall thickness of cylindrical shells from Reference 1,UG-27(c)(1).

UG-27(cXI) requires that one of thc following applicability criteria be met:

-4 "ube "ClanndA & 8" A value of 1 Indicates the applicability

9 i) II (la

( )~iJ=2

'I

-Manway Nozzle" criterion Is met. A value of 0 indicates the applicability criterion isnot met.

(Pt S 0.3S5-Swh I where 0.035 0.625 I(0.34' 034 9.8!

l0.6o S= Iksi E =E=0.85 a = 0.625 in r9.375 In r.8 1081 0.313) 1% 9)j 9.5)~

Pt = 191 psi Detennine the minimum required wall thickness.

S-E - .6-P, where t, required wall thickness Pt design pressure r, a hside radius S aa maximum allowable stress E joint efficiency (0.03 *ube 0.756 'ChannedA & B" In.¢l 1 0.232 in

,a263J WManway Nozzle

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Calculation No.:

FAIM PR Prepared By: I ILa.._ 01080309Jl -1 RevisionNo.: 0 MPR Associates, Inc.

320 King Street A1exandria VA 22314 Checked By Re. mfew'fi~ J Page No.: 15 Summarize the results and compare to the actual wall thickness.

TI- for IE I..rows(+c),)

al4- if(tr.Wyi5 taz.OIk-nok) saack(R1.iaugnmint(lj,t, inje + fn.a))

• Locion. 'Reqtured? 'Acutua "Result"

- "Thickness" "Tickne" TI a M-rube" 0.0)3 0.03S NC ranwdA & B& 0.756 0.625 -Not Mk" "Ok" "Ine,a

• Jnla t & Out. Nozzle 0.232 0.625

'anmvy Nozzle .263 0.313 'Ok")

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~ Page C-17 of C-38 5x f n _-_d Calculation No.

AM P C Prepared By: ¶A _ L 0108-0309ilh-1 MPR Associates, Inc. Revisin No.:

320 King Street R Alexandria VA 22314 Checked By: R. ,Ae .( Page No.: 16 4.3 nlange Bolt Tensile Area The flange design bolt load is calculated with Reference 1,Paragraph UA49. The basic gasket seating width is calculated in accordance with Reference l, Table UA-49.2. Use Sketch lc, Column ll for the channel gasket and Sketch la, Column 11 for the manway gasket.

Note: The inlet and outlet nozzle fange bolts are not included in the evaluation because the net and outlet nozzle flanges are standard ANSI B16.5 flanges for attached piping.

See Section 4.6 foran evaluation of the Wnlet and outlet nozzl fanges.

The basic gasket seating width for the channel and manway gaskets are:

rwg + I;fVg

+ Nil )

2 '4)1 II n(25) i 12 (ChannedlA &

b=0.75 i 2Manivay 1 2

where wS = 0.5 it 2 = 0313),

J = 0.125 in w8 + Ngl = 0.2S5i NS =0.5in 1

The effective gasket seating width is calculated with Reference 1,Table UA49.2.

bl:: +b S90.25Sinb 0.

1

) b (0.25 0.433) i

=( ManwOy whore b . (a2)in (0.75)

Note: The gasket width for the manway Is klss than the actual width and so the gasket seating load calculated belotv is underestimated The approach used is considered reasonable fore full face gasket fr the purpose ofsizing the flange bolts.

The location of the gasket load reaction is calculated with Reference 1,Table UA-49.2.

. r I f(b, % O.25-i ,drodg, b;)

(67.375 12 . ('hneA&- )

20.634 " ManwayZn rd . Jr375) 08=(67.875) ) h where 20 ads21.5 Jt

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• _.6 No.:

RIU MP =-Th~bCalculation Prepared By: _ 9 0108-0309-jlh-1 MPR Associates, Inc. Revision No.: 0

320 King Street Chedced~y~iaa6eq Pgf.1 Alexandnia VA 22314 sie-By -. Page No.: 17 The nange design bolt load Wmn is (UA-49(a)(1) formula (1)):

H 680959) b 12 (OChanndA & B' )

Hi =- (G atP 63869 'Manwwy H (70 749l I. (*ChanndlA & B lip,'.= 2-b.-jr G.-m-P 70769 b W "Manway" (751708 (bChannelA & B' )

Wtg.- HJ + Hp, = u,hf 12 = a WMI134637) k ManwayV' /

where n , . (35) Pi = 191 psi The flange design bolt load Wm2 is (UA-49(a)(2) formula (2)):

(42333o lb (ChannelA & B")

Wm2her - -eY8j Ibf208 12= *anway'

'B000 where yg (8000) P; The actual bolt tensile arca is:

(3017) I in

.2 Ab = t2= (vChanndJA & BR )

Abie nbj-At, "Manway" )

<16.03) t(0.419) .2 whlere = (2) 0.693 The required bolt areas Aml and Aa are:

Am J (3007) b 2 A,nl :=

i

-1 Sb = 5.39 1 12=

2 ( zanme!A & B- )

Mana& )

Amz,=W2- wn A,2-(1-3i,3 2 I2 ('ChtannelA & B- )

12 Zm 3.37 ) -Manway' w~here SC -(2S()

S 2 5i Sb=25)s

)ts

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!-XC-SW-MEE-1882 *?'e 0 Page C-19 of G-38

^- 1 e~

W7 A.

Calculation No.:

k M Vl K Prepared By: )Ik - 010&3-093jlh-1 MPR Associates. Inc. Revision No.: 0 320 King Street CiP Alexandria VA 22314 Checked By: A pw 'Pe Page No.: 18 The required bolt area Am is:

i('Channel A & B A.,:= nax(AIj,Am2j) Am 30 )n (5.39J 2Manway" Summarize the results.

72:= for le 1..row(An) a; i-f(A(( S Aboknok) stack(R2 .agnien412. A,, t in.Ab + 12,a))

OLocadon" wRequirar uActuar wRauet

'Bolt Area' "Bolt Area' n =in. W2" tun ^ 2'

• ChanndAdB 30.07 30.17 "Oko 5.39 5Manway 1663 "Ok)

The flange design bolt load is thc maximum of the load for operating and gasket seating conditions (Reference 1,Paragraph UA-49(c)). From Reference 1, UA-49(c), the bolt load for operating conditions is Wm,. The bolt load for gasket seating conditions is:

" 752954 -(ChanndA& 0' )

Wai (A . 'Manway) t27.5219 The flange design bolt load is the maximum of the load for operating and gasket seating conditions.

(

Wj ~ma~ i 1 a ,,

W (752954.) l 275219 =

'"ChanndA&

"Manway" BJ

)

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M Calculation No.:

FAIMPR Prepared By: I \ > 0t08.0309 jlh-1 MPR Associates. Inr. Revision No.: 0 320 King Street Alexandria VA 22314 Checked By: g p Page No.: 19 4.4 Channel Tlange Evaluation Flange moments for the operating and gasket seating conditions are calculated with Reference I, Paragraph UA-50. The flange is evaluated as a loose type flange because the material strength of the channel is less than that of the flange ring and because the ASME Code allows this approach (Reference.

1, Figure UA-48 and Paragraph UA-48(a)(3)). Evaluate the criteria for applying the loose flange

{

evaluation.

S0- o CAx g6= 0.625in 81 5.'

A value of 1 Indicates the applcability criterion ismet. A value of 0 indicates the

!5300 Pi 5 300-psi

= I] applicability criterion Isnot met.

"channel where Bchonl = 66.25 it =106 go PI = 191 psi Operating Condition Calculate the moments MD, MT, and MG with Reference 1, UA-47(b).

HD 4 (=Camle HD = 658408if lHr& = Wmli rha-am chana HG = 70749Wb See Reference 1,UA-47 l HT:= HJ - HD Hr = 22551 Ibf where where Wn,,

• 751708 1b Hcludnel ' 60959 Of

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Prepared By 0108-0309jlth-MPR Associates. Inc. VI Revision No.: 0 320 ring Street Checked Alexandria VA 22314 R/;$p Pg o:2 bchannet Bchannel 1 See Reference 1, Table UA-50; the flange Is

'D = I.Sill hD 2-G conservatively treated as a loose type Rlange, since the channel material Is weaker than bchannel ichannel the flange material.

f1G Ic 2 hG = 0.94in hD + hC; liT w 1.22in 2

where channel = 69.25 In ehallne -67.3375 in MD -- HDt-D MD = 82301 ft lbf MG := HGhG MG = 5527Jt lbf MTr: HRThT MT = 2290fpibf The total moment is:

Mop:= MD + MC + MT Mop 90119 f* lb Gasket Seating Condition From Reference 1, Paragraph UA-50, Equation (5):

Jugaslz-Wsa Mgs2 r

-WStMg~ke, .('chalnnel -&Gannei) - 58825 ft-lbf

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• dMPR MPR Associates. Inc.

Prepared By: - - 0108-039jth-1 Revision No.: 0 320 King Street Checked By: ,v Page No.: 21 Alexandria VA 22314 Flange Stresses Thc maximum moment is:

M := max(Map.Mgaske:) M - 90119J.Ilbf The flange stresses from Reference 1, Paragraph UA-51(2) are:

AchKncl Reference 1,Paragraph UA-47(b)

Kc:- danel where Ac = 71.125 in chan I 66 25 in t, ude 1 Kch _Iog(Kchf1 Y := .66845 + 5.71690. Reference t, Figure UA-51.1 K- I 2 _I y = 2.18 Y-M t2-0 Sg=:psi SH :-=O-psi Rearrange the equation to calculate the minimum required thickness of the flange.

y.M lfr.lange =- a 5.035 in tr.jlage where S-fC C -17.Sksi The allowable stress for the tangential stress, ST, is from Reference 1,Paragraph UA-52(a)(3)

The actual flange thickness is = 4.63 In. Add the results to the summary table T1.

TI := stack(TI.augqmnt("ChanfleFlae trfl'fjIwge

• Lv#,*ad + in,.Jflrtfae8, S I

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FAIM PR MPR Associates nc.

Prepared By: It_ 0108-0309.jlh-1 Revision No.: 0 32 KWngSreet treete~Wz2 CheckedSBy:

Alexandria VA 22314 Chd R. Page No.: 22 4.5 Manway Flange Evaluation The manway flange has a full face gasket, which cannot be evaluated with the rules of Reference I, Appendix n, Part A. Refercnce 1,Paragraph UA-56 references Paragraph UA-6(b)(2). This provides the required flange thickness for a spherically dished cover with a full face gasket.

t r.mnway := 0.6. Isj I p 58 in A tam a

+ -9W-y-"Cnk

-B _

Sfuatwn" mans ay ttanway rt.maray 1.44 in where PI = 19) psi AManway =25 isa bcManway = 22 75 in B - 18.625in Sf =1J7.S tsi nSuntJMWI Tbe actual flange thickness is i . 2in. Add the results to the summary table Ti.

4 T := stac(TI autglnsen:("ManwavyFlame .tr namvay 4 in-I0ffult* ini1f(Irnmaniwsays Iftionl, .ny-okno,)))

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_,Prepared By: _ L Cacutlation No.:

m rPpr y: 0108-0309-ih-MPR Associates, Inc. RevisionNo.: O 320 KWng Street CevisionBN, Alexandria VA 22314 ChedcIedBy . %ePRd Page No.: 23 4.6 Inlet and Outlet Nozzle Flange Evaluation Reference 1.Paragraph UG-44(a) recommends that bolted flanges to external piping conform to a recognized standard. Such flanges may be used in accordance with the pressure-temperature ratings of the standard.

The inlet and outlet nozzle flanges are ANS[ B16.5 standard flanges with a 150# rating (Refcrcnce 4, Grid C-2). At a design temperature of 2001F, the allowable pressure is Pjj0o.a, = 240 psi (Reference 8, Tablc 2).

Summarize the results.

'Location' 'Pressure' *Desgn Mault"

• Ragngw "Pressure T5n Ynet &OutletNozzle Flnge' PM 1 aiow-P 1 . si P#+*Psi O(P, gPisadliowok-na8k),

'Location' "Pressure "Dsign- "Resull" Raing" 'Pressare' "

T5 =

'psi' "psi "

'hsnleg & Ourde Nozzle Flange' 240 191 'Ok' )

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.5 ,8-SW-MEE-1 882 tP) 0 Page C-25 of C-38 Calculation No.:

FM IMEPR Prepared By:

• 010O8-0309-jlh-1 Revision Rn. No.: 0 MPR Associates.

320 King Street k B Alexandria VA 22314 CheckedBy: , c;. PageNo.: 24 4.7 Minimum Ihickness of nFat Cover Determine the minimum required wall thickness of flat heads from Reference I, Paragraph UG-34, Equation 2. The minimum thickness for the channel cover is calculated for operating conditions. The minimum thickness for the manway cover is calculated with the fonnula for no edge moment, because the manway uses a full face gasket.

1.78 Wmi *ho Ir.fla :=

dchatnel +

I

~Sj .(dWW~d C*Manway 3

I I ( ChzanneIA Y II bc mawa where triat required wall thickness d a flat plate diameter, for which the mean gasket diameter is used C geometry dependent factor from ASME Code PI design pressure SUM maximum allowable stress W bolt load hb M gasket moment arm bc flat plate diameter, for which the bolt circle diameter is used 2'ChanndA & r)

= 1.188) 2= 'ManW'y Where P, - 191 psi bcmaney a 22 75 in sflat a (M175i1s channe! a 67.38in Wh m = 75J70818 f C =0.3 hG - ° 938i

.0.25J The actual cover thicknesses are ff= (619) bn.Add the results to the surnmary table Tl.

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IRs Prepared By: ,0108-0309jlh-I1 MPR Associates.Inc. C B Revision No.: 0 AJexandriaVA 22314 2 ed 4 y:5 Page No.: 25

.-I1for i e L.. o~r.WrJ~ar) a f-fif(l.fta:. :5 Iji ,ok ,11olk) xtack(TI,augmeizn(13,tr,,qla: in.tJr47al iana))

The channel cover plate is grooved for the gasket as shown in Reference 1, Figure UG-34(k). The requirement for the cover plate thickness at the groove is provided in Reference 1, Paragraph UG-34(d).

1.78 -u,j AG 4.,gwove dachanne,' 3 Reference 5, p. $ shows that the gasket groove in the cover plate is in the Clad materjal and that the groove does not infringe on the cover plate thickness of - 6.19 in that is used in the above evaluation. It is concluded that the thickness of the cover at the gasket groove is acceptable without further evaluation.

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54 AP LI r Prepared By: I 010W-309-Jlh1-MPR Associates, Inc. RevionNo.: 0 320ring Steet CheckdNo.: 26 AlexandraVA Cheked By: Page No.: 26 4.8 Reinforcement Area Evaluate the reinforcemcnt area for the inlet/outlet nozzle opening in the channel and the manway opening in the channel cover. The reinforcement area requirements are in Reference 1, Paragraphs UG-37 (channel) and UG-39 (channel cover).

The required reinforcement area is:

A, :=

idInl ariqwnaeJet 1&75e A (=14J7)

(.35.92J

.a2 14 3

("InelOudet Nozzle"?

'Manmwa )

where id 1875in- 4fanway 11 Clcaaw = 0.756in tr.flat 391 in Define functions to calculate the reinforcement area available in the vessel wall and in the nozzle (Reference 1. UG40).

AI(EsF-,tF tj.t)  : al - (Ep-t -F-tjd a2 4- 2-(El-I - F.iJ)(t + ti) nx(ala2,0) 2(ft~ttn.t)- al 4 (.r -t) 5t a2 i- (in - fI n+ 2te) nmx(O,mrn(a1,a2))

where El W joint efficiency for a longitudinal weld if it passes through nozzle; 1 otherwise t a nominal vessel wall thickness F a correction factor for variation in pressure stres; 1.0 for this evaluation tr required thickness of vessel aM d diameter of fnished opening W nominal nozzle thickness tn tin W required thickness of nozzle to thickness of reinforcement pad

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F _S-. ,

Calculaton No.:

FAIMPs_e

_, e Prepared By: \ " L 0108-0309jth-1 MPR Associates, Inc. Revision No.: 0 320 Mig Street Checked By 2p Alexandria VA 22314 e e Page No.: 27 Calculate the linit of reinforcement parallel and perpendicular to the vessel wall (Reference 1, Paragraph UG-40).

n=(id1,,t, 2 , 1 +

UG-40(b)(1 )&(2)

I id..

2 J"'h.manel "

"M

' = 1(8

75) 14= ('InletOudet Nozzlc" )

ar= 18 i 4Manwy 4:=

rmin(Zs5taChwrndZ5ralkt tlr 5 ita .

• 2.n52.5 tpat)

+ 0-in) UG-40(c)(1 )&(2)

,Per = ( S) n 14 = (PinteMlalki Nozzay')

0.78 'Manway where 0o.03S (0.68s Tube" 0625 65 CMhairnelA & B" 0.625 in id j& 75 - "'Inle& Out. Nozzle 0.313 J8 "ManwayNozzle" )

tJ'at,6,,,, = 6.19 i npad 0.625in Calculate the reinforcement area Al.

Al A l(J, teba~r I 9r.ak,,,,,=' dtinl~a Webi)

UG-40(d)(1))

Al - 3914 ("Inet/Outlk oz' (9,) 2 1

Manwanm where . L1 9 1IinI*. 1- = 0 7%9 ha

- .gcanl - - rL yc7.wiarl

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_.w v *Calculation No.:

M m PR Prepared By: \ S 03O9-i 010&8ao-MPR Associates, Inc. w Revision No.: 0 AlxandriaVA22314 - Checked By:., = i Page No.: 2B Calculate the reinforcement area A2.

A2 :u rA,2(ta.,,.. .trM.ty,,

'r .ta - o 0.i l) G40d LPG-4D(d)(2)

(.229 ) 2 14(nlet/Oalld NozZJe" )

- n0.077) J  % jManwayg J where t Irtcj =0.232in IreyIm. = 0.26314 tpd = 0.625 in Calculate the reinforcement area of the reinforcing pad, A5.

A. 9[pad' (d,, - 311 )]

A 5= (6°25in2

(

t "InleilOulte Nozzle"

'Manway UG-40(d)(3) where odpad 30in Lp a ir 75 in od la = 20 in The total area of reinforcement is:

A, 01 :w Al + A2 + A5

-39.63)

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FAM PMR Prepared By: .1s\-- 01 08-0309-jlh-1 MPR Associates, Inc. jl Revion No.: 0 Aexandria VA 2314 Checked By: A' Page No.: 29

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5-gC-SW-MEE-1882 Page C-31 of C-38 fi.r-L A>-.- as VI-r - -F-- W-u Wki NR zMEA MKI PveparedCalculation Prepared By: 3 BA W No.:

011080309-jh.11 MPR Associates, Inc. By Revsion0No.: 0 320 King Street CheckedNo.: n 0 Alexandria VA 22314 cAomBy: R. ,m Page No.: 30 4.9 Tubeslieet The ASME Code (Reference 1) has no requirement for the thickness of the tubesheet. Reference 2, Data Sheet indicates the heat exchanger was designed to the TEMA R standard. Use the 1968 TEMA R standard (Reference 12) to determine the minimum required tubesheet thickness.

The minimum tubeshect thicknesses for bending and for shear arc (Reference 12, Paragraphs R-7. 122 and R-7.123):

Ib d ' *1r 0.31-DL Ps tshear I od Si*

_-_d where t bead = minimum required tubesheet thikness for bending 6sear z minimum required tubesheet thickness for shear Fm thickness l multiplier GC = IDof pressure vessel Pts = tubesheet design pressure S's = tubesheet allowable stress at design temperature DL = equivalent diameter of tube bundle (4'arealcircumference) ock = tube OD W tube pitch Tle tubehseet is integral with the shell and the channel head, i.e., the tubesheet is welded to both structures and benefits from the stiffening they provide. In addition, the tubesheet is stationary (there is no shell expansion joint). Accordingly, the parameters Gc and Fm are determined with Paragraph R-7.141 of Reference 12.

Ge can be the ID of the channel head or the I) of the shell depending on the calculation. Since the two diameters are equal (id..Mz = 65 in and id =65 in), set G. to the ID of the channel.

0 5i Gc=65kIS cc IdChgasn.= l

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• zM PR Prepared By .I \k 01O03O9-,h-1 MPR Associates, Inc. Revision No. 0 320 King Street ChYe ya o Alexandna VA 22314 CheckedBy: ,  ? Page No.: 31 Calculate the thickness multiplier, Fm, with Reference 12, Figure R-7.141 for integral stationary tubesheets. Calculate the ratio of wall thickness to ID for both the channel and the shell. Use the smaller of the two ratios to calculate F. for conservatism.

raios 1:= rnios =1 k0.008)

I t,

_wI$

where a =0.625 in idChannel = 65 in = 0.5An ChunneE Id$ = 65 in rmaz: rnin(rgnos) r,,, = 0.008 F7 4 1(x)= I1I # x<0.02 in 4(a5).(0 I) ]if0.02 <0.05

-,I 0.8 if x>0.0S F. := F7.1 1t(rn,) F, = 1.000 Tlhc tubesheet design pressure, Pt5, is the the hydrostatic design pressure modified by Rcfcrence 12, Paragraphs R-7.153 and R-7.154. Calculate the modified tubesheet design pressure. This requires equivalent differential expansion pressure from R-7.151 and the equivalent bolting pressure from R-7.152.

Equivalent Differential Expansion Pressure-R.7.151 Calculate the equivalent differential thermal expansion pressure.

Jiff Shell has no expansion joint

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FMM PrK Prepared By: 5a O 01080309jlh-i MPR Associates. Inc. RevisionNo.: 0 320 land StVeA2 Checked By: , , 5 , Page No.: 32 The tube (sub t) and shell (sub s) differential temperatures for thermal growth are:

u,* (T..1- 70.r) 8, - 30.57F e, a Tamm, - 70F 6 t9 '36.5 F where Taq.t = 100.57F Ta~w= 106.5 F Calculate the constant K.

Kn E5s-.-(od - t5) K =0.734

-EIta- .N:-(odTb - aT) where E5 ' 2934x 10 psi od5 = 66 in El = 1.538 x 10 psi tarlk = 0.035 in N. = 3400 °Tubr = 0.75 i Guess that the required tubesheet thickness is t,, = 1.966 in. Calculate the constant Fq.

Fq:= lnu" .{ 5I (. 06) C300 ts-Es K-L-Ej,5

(

(Gcr _

Fq = 5.2 43 where L - 304.5 in E.=u2934x 10 psi GC = 65 in The differential thermal expansion equivalent pressure is:

4-J-E,-I, (a59 -at)

Pd =-I57psi (ads - 3 s) (1 + J-K-Fq) where as-S. 73xl 1"6 'n at . 4.65 x 1l7 6 in

-6 F - iF

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0108-0309-jih.1 Revision No.: 0 320 King Street Alexandria VA 22314 BY: , AJ

.9p5o Page No.: 33 Equivalent Bolting Pressure-R-7.152 Since there is no bolting on the tubesheet periphery.

Pe, E0-psi P'5E 0.psi Effective Shell side Design Pressure-Z-7.153 fS. 1I- (4 ds WTue

)C 2

f, =0.5473 DJ

• GC Shell has no expansion oint

[0.4.J{I.. + K(l.S +f$)] -([I t(- P5. = 37.16 psi I +FJ-K-rl,

.. , . 1 . i. . .

where P, = 150 psi PI- - PdI 121 12.3 37.16 0

Pal ; PsB +d P I Pa, =

123 psi 628 3Z16 12 1 IPSl-P&I pshed1 =:-ir ma(Pa ,) Pshell = 371 ps sz =37.16pst

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WAd~N~b ' Calculation No.:

FAM PR Prepared By: 3 O 0108-0309jlh-1 MPR Associates, Inc. A Revision No.: 0 320 Klng Street __ __ aS_

_3 Alexandria VA 22314 Checked By: R* Page No.: 34 Effective Tube-side Design Pressure-R-7.154 Note: The formulas i this section assume P. Is positive. Le., there is no shell expansion joint and J=1.

fA /- Nt(TdGubera t, - 0.6279 Pr: l. 0.4J.)K..(I..s + ft)] Pi = 64.01 psi

{ I + J.K-Fq I

'Paz:= 1 (Ps. +P&+ P]

2 ' l' Pa2 =

(38.29~I829 (64.01J Ps, lP-+ PBrI fgube:= fax'(P.2) P1,1,, = 64.01 psi Design Pressure for Tubesheet (see definition of P In Reference 12,7.122)

PHs:= nmax(Plabe,P5hll) Ps - 64.01 psi Tuibesheet Thickness Fm-Gc Hi;;

tbtndT 4 tbend = 1.97Jn where St: 17.5 s Drawings are not available to calculate the parameter Di. Approximate DL using the area and perimeter of a circle with diameter G,. This is a conservative approach, since the ID of the channel head is larger than the tube bundle diameter. Also, using a circle with diameter Gc to calculate the perimeter is likely conservative since it is judged to be smaller than the tube bundle perimeter as shown in Reference 12, Figure R-7.123.

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,S-,9SW-MEE-1882 ),,.' ! Page C-36 of C-38 n &,dA -ne ^ I Calculation No.:

• 0M PR Prepared BY: S 0108-0309*-l MPR Associates, Inc. , / / z Revision No.: 0 320 King Street 4Checked ,a Alexandria VA 22314 B:Page No.: 35 DL = 65 in

-rGc 0 31

. -DL Pis t tshcar = *- shear 0.29 in odrube Sg4 I _ W Pi where Pt= In t

rq.ts := Max4bnd.lshAr) freq. = .97in Verify that the guessed value and the calculated value meet the criterion of Reference 12, Paragraph 7.151, variablc T definition.

II 1iwq.ts -

1 r as I<<I.5'V-% o-- i A value of 1 indicates the cnterion is met.

I Ireq.ts I A value of 0 ihdicates the criterion Isnot met.

The actual tubesheet thickness is us= 3.5 in. Add the results to the summary table T1.

Ti := stack(TI,augnent(-Tubeshee( trtqts* injtis + ini(t;eq5tts t sok.no4)))

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Calculation No.:

01IB.0309.jlh-1 Revision No.: 0 320 King Street C Alexandria VA 22314 CheckedBy: /e '50AJ PageNo.: 38 4.10 Seismic Evaluation Channel Cover, Cover Bolting, and Channel Flange Reference 5, Paragraph 7B.1 determined that the equivalent pressure load on the cover from seismic acceleration is Pocsh = 24 psi. This is Pe

• PI P =1.3 % of the new design pressure of Pi = 191 psi. It is concluded that the seismic loading on the channel cover, cover bolting, and channel flange is negligible and that no further evaluation is required.

Channel Head and Manway Cylinder Section 4.2 of this calculation determines the channel and manway required wall thickness for the design pressure. The limiting stress in determining the minimum required wall thickness is the hoop stress.-

eismic acceleration produces longitudinal membrane and bending stresses. lt isconclueid that the seismic acceleration does not affect the minimum wall thickness calculation of Section 4.2 and that no further evaluation of the channel or manway cylinder for seismic acceleration is required.

Manway Cover, Manway Bolting, and Manway Flange Reference 5, Paragraph 7.B.2 determined that the equivalent force on the manway cover from seismic acceleration is-Fq = 540 Ib. This is an equivalent pressure of: 'C,.

Pm= eq. Pegs = 1.61 psi 4 (mannawy) where ntanway

=2 0.634 in This equivalent seismic pressure is Prg.m + Pi .0.8 % of the new design pressure of Pi =191 psi. It is concluded that the seismic loading on the manway cover, manway cover bolting, and manway flange is negligible and that no further evaluation is required.

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5.0 REFERENCES

1. 1968 ASME Code,Section VIII, Division 1.

2. PSE&G VTD No. 301110,7/25/91, Auxiliary Heat Exchangers Westinghouse Instruction Manual.

3. Greenkorn and Kessler, 'Transfer Operations," McGraw-Hill Book Company, 1972.

4. PSE&G VTD No. 111008-05, EFCO Drawing No. NEN-15763, "Shell, Chan. & Support Details."

5. PSE&G VTD No. 316898-01, 'ASME Code Calculations for Component Cooling Heat Exchanger Modification No.Ij Unit," Original Issue.

6. Oarlock Gasket Product Catalog, available at web site:

http:/lwww.garlock.netluploadfcatalogslGSK%203- 1%200asket%20catalog.pdf.

7. E. Avallone & T. Baumeister, "Marks' Standard Handbook for Mechanical Engineers,"

McGraw-Hill Book Company, 9th Edition.

8. ANSI B 16.5 (196 1), 'Steel Pipe Flanges and Flanged Fittings."

9. PSE&G VTD No. 320478, Equipment Specification No. G-676454, "Auxiliary Heat Exchangers," Revision 1.

10. PSE&G VTD No. 117638-04, EFCO Drawing No. NEN-B-15763, "Tubesheets.".

II. 1992 ASME Code, Section 11, Materials, Part D, Properties.

12. TEMA, "Standards of Tubular Exchanger Manufacturers Association," 5th Edition, 1968.

13. Form U-1, Manufactured by Engineers and Fabricators, Vessel No. S-15763-A, National Board No. 1148.

14. 2001 ASME Code, Section 11, Materials, Part D, Properties.

Document Control Desk LR-N05-0446 Attachment 1 10 CFR 50.55a Request Number SC-RR-W03 Proposed Altemative InAccordance with 10 CFR 50.55a(a)(3)(i)

Altemative Provides Acceptable Level of Quality and Safety Enclosure 2 S-C-SW-MEE-1 882, Salem SW Heat Exchangers - Suitability for Operation at Higher Pressures, Revision: 0, Attachment D, MPR Calculation 0108-0.309-jem-1, "Component Cooling Water Shell and Tube Heat Exchanger Channel Analysis," Revision dated 1/27/050.

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Attachment D: MPR Calculation 0108-0309-jem41, "Component Cooling Water Shell and Tube Heat Exchanger Channel Analysis," Revision 0

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• A MPRI 320 King Street Alexandria, VA 22314 CALCULATION TITLE PAGE Client:

PSEG Nuclear Page I of 15

(+Attachments)

Project: Task No.

Salem SW HX Re-Rate 0108-0418-0309-00

Title:

Calculation No.

Component Cooling Water Shell and Tube Heat Exchanger Channel Analysis 01 08-0309-JEM-1I Preparer I Date Checker / Date Reviewer & AIer Date Rev. No.

Ja0me MCo s /o b Coward0 "James Moroney Teresa Tellow Robert Coward O QUALITY ASSURANCE DOCUMENT This document has been prepared. checked. and reviewed/approvcd in accordance with the Quality Assurance requirements of I 0CFR50 Appendix B. as specified in the MPR Quality Assurance Manual.

MPR-OA Form QA-3.1-1. Rev 1

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• OMPR 320 King Street Alexandria, VA 22314 RECORD OF REVISIONS Calculation No. Prepared By Checked By Page: 2 0108-0309-JEM-1 9 a Je Revision Affected Pages Description 0 All Initial Issue lf te c Note: The revision numberfound on each individualpage of the calculation caies the revision MPR OA Forn OA-3.1-2. Rev 0

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• XMPR .

320 King Street Alexandria, VA 22314 Calculation No. Prepared By Checked By Page: 3 01084309-JEM-1 9c. '.t V  % Revision: 0 IJ Table of Contents 1.0 Purpose................. 4 Lo Summary of Results ...... 4 II 3.0 Finite Element Model ...... 4 3.1 Model Geometry ...... 4 3.2 MaterialPropertes ...... 7 3.3 Boundary Conditons ......

4.0 Analysis ...... 12 4.1 Analysis Results ....... 12 5.0 References ...... is A PlasticAnalysis Deflection Data ...... A-1 B ANSYS Output Files ...... B-1 MPR QA Form GA-3.1-3. Rev. 0

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320 King Street RIM , R,Alexandria, VA 22314 Calculation No. Prepared By Checked By Page: 4 01 08309-JEM-1 g* Revision: 0 1.0 PURPOSE This calculation documents a finite element analysis of the Service Water side of the Component Cooling (CC) Heat Exchangers Nos. II, 21, and 22 at Salem. PSEG Nuclear is currently re-evaluating the Salem Service Water (SW) system heat exchangers for an increase in design pressure from 150 psig to 200 psig. This analysis is being performed as part of that effort. This elastic-plastic finite element analysis calculates the collapse pressure of the heat exchanger channel.

2.0

SUMMARY

OF RESULTS Using the methodology of Reference 7, Appendix 4, 4-136.5, the maximum allowable pressure for the SW sidebf CC Heat Exchangers Nos. I 1, 21, and 22 is 267 psig. This is not a certification that the Heat Exchangers meet all applicable ASME B&PV code requirements.

3.0 FlNnE ELEMENT MODEL A three-dimensional finite element model of the CC heat exchangers "A" channel has been prepared to calculate the collapse load of the heat exchanger head. Note that the "A" channel is larger than the "B" channel. Therefore the results of this analysis are bounding for both channels.

While this calculation uses a methodology described in the ASME B&PV, it does not certify that the CC heat exchanger is in compliance with all ASME B&PV requirements.

The finite element analysis was performed using the ANSYS general purpose finite element computer program Version 8.1 on a Sun Microsystems 280R server running the Solaris 8 operating system. The ANSYS installation verification is documented in QA-8 I-I 3.1 Model Geometry The model geometry is taken from References I through 3. Channel UA" is modeled along with approximately 2 feet of the heat exchanger shdl. Note that this section of shell is not being evaluated, but is included for boundary conditions only. In addition, the cover and nozzle flanges are conservatively not included in the model. Scoping evaluations indicated that these components do not significantly impact the behavior of the channel shell. No credit is taken for the structural strength of the tubesheet clad.

The model is a three-dimensional half model, with the axis of symmetry at the along the heat exchanger axial length at the nozzle centerline. Figure 3-1 shows the model geometry. The model is meshed with 3-D solid elements with 10 nodes (ANSYS Element SOLID45). Figure 3-2 shows the model mesh.

MPR OA Form GA-3 1S3. Rev. 0

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320 King Street UIM P R1 Alexandria, VA 22314 Calculation No. Prepared By Checked By Page: 5 0108-0309-JEM-1 -!r.IRevision: 0 AN I. . -

CCW HX Channel Head A Figure 3-1. Model Geometry 0

MPR QA Fm.: OA-3.13. Pwov.

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320 King Street FAIMPR Alexandria, VA 22314 Calculation No. Prepared By Checked By Page: 6 OIOS-0309-3EM-1 li r Revision: 0 AN 44j'y; --ii "; .;,%

• `. .i si ,!'.;'i .:.. '. '. I.

CCW HX Channel Head A Figure 3-2. Model Mesh MPR GA Form OA-3.1-3. Rev. 0

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320 King Street W MPR Alexandria, VA 22314 Calculation No. Prepared By Checked By Page: 7 0108-0309-JEM-1 I ' _ Revision: 0 3.2 MaterialProperties Table 3-1 shows the component material properties used in this analysis. All component materials are taken from References I and 3.

Table 3-1. Model Materials Component Material Channel Nozles SB-171 90-10 Cu-Ni Partition Plate

! Chiannel'Flange- >":Ki;;; . SA-105-11 Tubesheet Heat Exchanger Shell SA-5 15 Grade 70 Nozzle Repad To properly account for the redistribution of load and potential concentration of strain for loads that produce stresses beyond the elastic limit, elastic-plastic material properties were included in this analysis. The behavior of the channel shell is of particular interest. Therefore, a stress-strain curve was developed for SB- 171 90-10 Cu-Ni. Bi-linear stress-strain curves were used for the -

carbon steel portions of the model (SA-150-11 and SA-515 Gr. 70). Key material properties used in the stress-strain curves are shown in Table 3-2 (Reference 4).

Table 3.2. Key Material Properties Material Yield Strength Strain at Yield Ultimate Tensile Maximum (ksl) Strength (%) Strength (ksi) Elongation (%)

SB-17190-10 15 0.5 40 30 SA-105-11 m 36 38 0.5 0.5 70 70 30 21 SA-515 Gr. 70 The stress-strain curve developed for S-1 71 is based a standard stress-strain curve for SB- 171 90-10 Cu-Ni (Reference 5). 'he following adjustments were made to this curve:

• The yield strength point was set at 15 ksi and 0.5% strain.

• The ultimate tensile strength (UTS) point was set at 40 ksi and 30'/o strain. All points on the curve between the yield strength and UTS points were scaled down based on the ratio MPR OA Form GA-3.1-3. Rev. 0

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320 KIng Street

• AIMPR Alexandia, VA 22314 Calculation No. Prepared By Checked By Page: 8 01080309-EM-l 6 ~9' r Revision: 0 of the curve UTS (49 ksi) and the minimum UTS (40 ksl) specified in Reference 4. The scaling equation used is:

S.4s =SY +(S. -SY)*( ~ S,

• All points on the curve were adjusted for temperature. The material properties shown in Table 3-2 and the stress-strain curve from Reference 5 are based on room temperature, while the CC heat exchanger design temperature is 200 17 (Reference 6). The adjustment factor used is 0.98, which is based on the allowable stress intensity values for SB-171 9M0 Cu-Ni at 100 OF (10 ksi) and 200 IF (9.8 ksi), taken from Reference 4, Section V1II Table UNF-23.

-; . X : 0 AlU points on the curve were adjusted to account for channel shell joint ef iciency of 0.85 (Reference 1).

The digitized version of the initial stress-strain curve taken from Reference 5 and the three scaled curves discussed above are shown in Figure 3-3. The stress-stain curve for SB-171 90-10 Cu-Ni used in this analysis is shown in Figure 3-4.

4-4 E . , t, ..... , , .- -Sumld Is Fi0i a co ,. cis 0.2 0Z SM~

Figure 3-3. Stress-Strain Curve Scaring MPR OA Frmn: OA;S 4. Rev. 0

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UAMM PR - wM Ad320 King Street Alexandria, VA 22314 Calculation No. Prepared By Checked By Page: 9 0108-0309-JEM-1 7  ; V r Revision: 0 40.000 s .000 30ec 25OCC I 20.00

-" -t 'I ,  ; It , I w v 7'., 7 . : - , :. , .

- j '.:

I I !-

to0ao 1.o00 a 005 C.1 0 Is 0.2 025 o3

'Sain

., . V\ .

Figure 34. Stress-Strain Curve for SB-171 90-10 Cu-NI 3.3 Boundary Conditions I Figure 3-5 shows the model boundary conditions. The model is constrained at the following locations:

• Transvcrsc (X-axis) motion is constrained at the model plane of symmetry.

• Longitudinal (Z-axis) motion is constrained at the heat exchanger shell.

• The edge of the partition plate engaged with the cover is constrained against vertical (Y-axis) motion.

• The nozzle end nodes are coupled vertically (Y-axis) to ensure they remain in-plane vertically.

MPR CA Form. tA-3.1-3. Rev 0

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F*IM PR 320 King Street Alexandria, VA 22314 Calculation No. Prepared By Checked By Page: 10 0108-0309-JEM-1 7_l Revision: 0 Hydrostatic end loads are applied to the nozzles and the channel flange. The hydrostatic end load is calculated as follows:

F.e = PA, K'r, where:

Pdr = Heat Exchanger Internal Pressure r, = Nozzle inside radius (Reference 1)

One half of this load (due to half-model) is applied as a pressure to the end of each nozzle and the channel flange.

The internal heat exchanger pressure is applied to all of the internal surfaces of the channel. The internal pressure applied to the tubesheet is modified to account for the misting volume of the tube penetrations as well as the stiffness of the tubes. Reference 8 calculates that the effective tubesheet pressure based on an internal pressure of 200 psi is 62 psi. This objective of this analysis is to calculate the collapse load of the heat exchanger channels. Therefore, a maximum pressure of 400 psi, which exceeds the re-rate design pressure of 200 psi, is applied. At an internal pressure of 400 psi, an effective pressure of 624(400/200)=l 24 psi will be applied to the tubesheet.

OR UIPR OA Forrn: OA-3. -3 Rev 0

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TowsAhee

. .:l . j,.

pei.

Ctafnd V Ples Pac c

jCby 1A Hy.10We b Law Auaw I CMW4 Pibap wm=W7 FO t fa& MO CCS HX Channel Head A Figure 3-5. Model Boundary Conditions MPR GA Fcm OA,-1-. Rev. 0

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PR, 320 King Street Alexandria, VA 22314 Calculation No. Prepared By Checked By Page: 12 0108-0309-JEIMI-1 I Revision: 0 4.0 ANALYSIS This calculation peiforms a Plastic Analysis of the CC heat exchanger channel using the methodology specified in Reference 7, Appendix 4, 4-136.4. This analysis does not attempt to certify that the heat exchanger meets the requirements of the ASME B&PV. Using the full stress-strain curve discussed above, a collapse load is calculated using the methodology described Reference 7, Appendix 6, 6-153. As the internal pressure is ramped up to a final arbitrary load of 400 psi, the deflection of the channel shell at a location remote fom discontinuities is plotted.

From this deflection vs. load data, a collapse limit line is plotted. The intersection of the deflection curve and collapse limit line is the collapse pressure. Per Reference 7, 4-136.4, the maximum loading of the component shall not exceed two-thirds of the plastic collapse load.

.4 - With the deflection vs. load plotted with the load on the ordinate, the collapse limit tine is determined by first calculating the angle between the elastic portion of the deflection curvc and the ordinate (e). The angle between the collapse limit load and the ordinate (0) is calculated as follows:

P= tanN'(2tane) 4.1 Analysis Results Figures 4-1 and 4-2 show the stress intensity distribution of the channel at 200 psi and 400 psi, respectively. Review of these stress distributions indicates that the channel shell stress is primarily membrane stress and that no plastic hinges have been formed.

Figure 4-3 shows the deflection vs. load curve and the collapse limit line calculated in accordance with Reference 7, Appendix 6, 6-153 (See Appendix A for data). This data is taken at a point approximately midway between the tubesheet and flange (axially) and midway between the partition plate and upper nozzle repad. This is where the maximum shell displacement occurs.

The deflection vs. load curve on Figure 4-3 had not yet intersected with the collapse limit line at a pressure of 400 psi. Based on this, it is conservative to assume that the plastic collapse load is at least 400 psi. Given a plastic collapse load of 400 psi, the maximum heat exchanger channel load is 2/3 * (400 psi) - 267 psi. The displacement and strain at other locations, including the highest stress region, were also evaluated using this methodology. In all cases, the displacement data and collapse limit lines were essentially identical, supporting the 267 psi maximum heat exchanger channel load.

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w w-. - 320 King Street PA M- R Alexandria, VA 22314 calculation No. Prepared By Checked By Page: 13 0108-0309-JEM-l Z , Revision: O ANSYSO 8.1 DEC 27 2004 11t48128 oIWALSOWSION TIHE-200 SINT i.230954IAVV)

HnX 91- :146.;534 mU .34 96 153503 13341 231a0 270131 308S7 3a609 CCH ILY ChanneL Read Aj Figure 4-1. Stress Intensity Distribution at 200 psi

.. EtSY Si.l OSC 27 2C04 lit4908.

KDAL SOWLTlaN B 42381 31Ita400

~U MX ChaneS3He7d4 Sres42.Intnsiy Ditriutio at40035s Figue MPR OA FoTr OA-3.F3, Rev. 0

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_Model Dt

- Lbl"eLIM 0 0.2 03 0.4 0.5 0.6 Displacenmnt gn)

Figure 44. Deflection vs. Pressure Data (Including Colapse Limit Line)

MPR QA Foam: QA Rev.0

-3.14

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5.0 REFERENCES

1. PSE&G VTD No. 111008-05, EFCO Drawing NEN-15763, "Shell, Chan & Support Details," Revision K. A

2. PSE&G VTD No. 108724-08, EFCO Drawing CD-15763, "Component Cooling Heat Exchangers," Revision G.

3. PSE&G VTD No. 117638-04, EFCO Drawing NEN-B-15763, "Tube Sheets," Revision B.

4. ASME Boiler and Pressure Vessel Code, 1968 Edition.

5. Boycr,HowardE.,Atlas of Stress-Strain Curves, Figure 16-71, ASM International, 1987.  :

6. PSE&G VTD No. 30110, 7125/91, Auxiliary Heat Exchangers Westinghouse Instruction Manual.

7. ASME Boiler and Pressure Vessel Code, Section VBI, Division 2,2004 Edition.

8. MPR Calculation 0 108-0309-JLH-1, 'Component Cooling Shell and Tube Heat Exchanger Service Water Pressure Rerate Evaluation - -ICCE5, 2CCE5, & 2CCE6." Revision, 0.

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MIMPR 320 King Street Alexandria, VA 22314 Calculation No. Checked By Page: A-I 0108-0309-JEM-1 ,f f j Revision: 0 A Plastic Analysis Deflection Data Table A-I shows the deflection vs. load data taken from thc ANSYS collapse load analysis.

Pressure Displacement (in) 0.60.. 0.0003::

i 1.00 0.0006 1.75 0.0011 2.88 0.0018 4.5S 0.0028 7.09 0.0043 10.89 0.0066 16.59 0.0101 25.13 0.0152 37.94' .0:0228 57.17 I 0.0342 77.17 0.0459 97.17 0.0574 117.17 0.06886 137.17 0.0800 157.17 0.0911 177.17 0.1021 197.17 0.1129 217.17 0.1235 237.17 0.1344 257.17 0.1452 277.17 0.1599 297.17 0.1807 317.17 0.2028 337.17 0.2259

-l357.17 0.2499 I 377.17 0.2851 388.58 0.3109 I 400.00 0.3386 MPR QA Form QA-3.1-3. Rev. 0

USER, RFSPONSIBLE FOR VERIFYING REVISION, STATUS AND CHANGES PRINTED 20051108 9-/CSW-MEE-1882 (4, o Page D-18 of D-19 OSht O- § °5 MPR Associates, Inc.

• AM PR 320 King Street 2 Alexandria, VA 22314 Calculation No. Prepared By Checked By Page: A-2 0108-0309-JEM-11 C /1 S t Revision: 0 Using this data, the slope of the elastic portion of the deflection line is calculated:

P 37.94 psi =1675.21b/in my 0.0226in The angle (e) between the ordinate and the elastic portion of the deflection line is:

6 = 90 - tan- (m,, 4 ) = 0.034 The angle between the ordinate and the collapse limit line is:

4, = tan (2tan(V)) =.068 MPR GA Form. OA-3 1-3, Rev. 0

ULP5,t R&SPONSIBLE FOR VERIFYING REVISION, STATUS AND CHANGES PRINTED 20051108 S-XC-SW-MEE-1882 ~eJ-j Page D-19 of D-19 W a-2as MPR Associates, Inc.

320 King Street Alexandria, VA 22314 Calculation No. Prepared By Checked By Page: B-I 01 08-0309-JEM- I .17 Jr Revision: 0 B

ANSYS Output Files -

a Filename Date Time Hcad.out 11/17/2004 12:57 Mmshcoarseep.out 12/20/2004 18:25 Headep.out 12/22/2004 19:07 Pst.out 12/27/2004 11:43 MPR CA Form: QA-3.1-3. Rev. 0