ML15075A344

NUH32PHB-0402, Revision 1, Thermal Evaluation of Nuhoms 32PHB Transfer Cask for Normal, Off-Normal, and Accident Conditions

ML15075A344
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Site:	Calvert Cliffs
Issue date:	03/10/2015
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To:	Office of Nuclear Material Safety and Safeguards
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NUH32PHB-0402, Rev. 1
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ENCLOSURE8 NUH32PHB-0402, Revision 1,Thermal Evaluation of NUHOMS 32PHB Transfer Cask for Normal,Off-Normal, and Accident Conditions Calvert Cliffs Nuclear Power PlantMarch 10, 2015 CONTROLLED COPY E-281Form 3.2-1 Calculation No.: NUH32PHB-0402 Calculation Cover Sheet Revision No.: IAR EVA Revision 8 Page: 1 of 65DCR NO (if applicable):

NUH32PHB-01 8 PROJECT NAME: NUHOMS 32PHB SystemPROJECT NO: 10955 CLIENT: CENG -Calvert Cliff Nuclear Power Plant (CCNPP)CALCULATION TITLE:Thermal Evaluation of NUHOMS 32PHB Transfer Cask for Normal, Off Normal, and AccidentConditions SUMMARY DESCRIPTION:

1) Calculation SummaryThis calculation determines the maximum component temperatures of the Calvert Cliff Nuclear Power PlantOnsite Transfer Cask (CCNPP-FC TC) loaded with 32PHB DSC at 29.6 kW without forced convection and alsoprovides the 32PHB DSC shell temperature profiles.

2) Storage Media Description Secure network server initially, then redundant tape backupIf original Issue, is licensing review per TIP 3.5 required?

Yes 0i No 0 (explain below) Licensing Review No.:This calculation is prepared to support a Site Specific License Application by CCNPP that will bereviewed and approved by the NRC. Therefore, a 1OCFR72.48 licensing review per TIP 3.5 is notapplicable.

Software Utilized (subject to test requirements of TIP 3.3): Version:ANSYS 10.0Calculation is complete:

QI Jianwei2015.03.03 14:15:52

-05'00'Originator Name and Signature:

Davy Qi Date:Calculation has been checked for consistency, completeness and correctness:

G UZEYEV z...DN: -n GUZEYEV Vyachersav, GUZEEV -G'U'ZEY'EVgýeN-n-W.hesav,

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ou=AREVAAMERICAS, Checker Name and Signature:

Slava Guzeyev V IachesdLII')

20V ..... .SW' Date:Calculation is approved for use:PATEL Girish__ o=AREVA GROUP,2.5.4.45=T1 1D2D8D4139956740417FCF, cn=PATEL Gidsh2015.03.03 16:14:20

-05*00'Project Engineer Name and Signature:

Girish Patel 5a3e0Date:I Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 2of65REVISION SUMMARYAFFECTED AFFECTEDREV. DESCRIPTION PAGES Computational 1100 Initial Issue All All1 Add sensitivity studies of the applying the solar heat Additional runload to the full circumference of the cask when transfer 1-4, 7-8,16- files markedin the horizontal orientation to address RAI 6-6 from 17, 50-52, with revisionNRC. The temperature term Tj is corrected to T'in and 63-65 bars listed inTables 4-8 and 4-9 in response to RAI 6-11 from NRC. Section 8.0 Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 3of65TABLE OF CONTENTSPage1 .0 P u rp o se .............................................................................................................................

62.0 References

........................................................................................................................

73.0 Assumptions and Conservatism

..................................................................................

93.1 CCNPP-FC TC Model ...........................................................................................

93.2 32PHB DSC Model .............................................................................................

104.0 Design Input ....................................................................................................................

114.1 Design Load Cases ..........................................................................................

114.2 Major Dimensions in the CCNPP-FC TC Model .................................................

114.3 Thermal Properties of Materials

.........................................................................

124.4 Surface Properties of Materials

..........................................................................

194.5 Design Criteria

....................................................................................................

195.0 Methodology

....................................................................................................................

215.1 CCNPP-FC TC Model ........................................................................................

215.2 Fire Accident

......................................................................................................

235.3 Effective Conductivity of Slide Rails .................................................................

315.4 Effective Thermal Properties of DSC End Plates ..............................................

315.4.1 Top Shield Plug Assembly and Top Cover Plate 315.4.2 Bottom Shield Plug Assembly 336.0 Results and Discussion

.............................................................................................

357.0 Conclusion

......................................................................................................................

488.0 Listing of Computer Files ..........................................................................................

50APPENDIX A Total Heat Transfer Coefficients

..................................................................

53APPENDIX B Gamma shield gap justification

....................................................................

56APPENDIX C DSC Shell Temperature

...............................................................................

59APPENDIX D Sensitivity of the Effective Density and Specific Heat of the Homogenized Basket ........................................................................................................

61APPENDIX E Sensitivity Study of Applying Solar Heat Load to Full Circumference of theCask in the Horizontal Orientation

...............................................................

63 Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 4 of 65LIST OF TABLESPageTable 4-1 Design Load Cases for 32PHB DSC in CCNPP-FC TC without FC ..............

11Table 4-2 Major Dimension of 32PHB DSC in CCNPP-FC TC model [14] ....................

12Table 4-3 List of Materials in the CCNPP-FC TC Model ...............................................

13Table 4-4 Stainless Steel, SA 240, Type 304 / SA 182 Type F304N [6-8] ...................

14Table 4-5 Carbon Steel, SA 516, Gr.70 [7, 9] ...............................................................

14Table'4-6 Gamma Shield, ASTM B29 Lead [5] ............................................................

14Table 4-7 Castable Neutron Shield, NS-3 [12, 15] .........................................................

15Table 4-8 Air Therm al Properties

[4] .............................................................................

16Table 4-9 Helium Thermal Conductivity

[4] ....................................................................

17Table 4-10 Thermal Properties of Homogenized Basket(')

[13] ......................................

17Table 4-11 Effective Conductivity of Top Shield Plug and Top Cover Plate ...................

18Table 4-12 Effective Conductivity of Bottom Shield Plug ...............................................

18Table 4-13 Effective Conductivity of Slide Rail ...............................................................

19Table 5-1 Decay Heat Load ..........................................................................................

21Table 5-2 Solar H eat Flux .............................................................................................

22Table 5-3 Distance between 32PHB DSC and TC Centerline

......................................

22Table 5-4 Thickness and Weights of the Top End Assembly

.......................................

31Table 5-5 Thickness and Weights of the Bottom End Assembly

.....................

34Table 6-1 Maximum Temperatures of CCNPP-FC TC @ 29.6 kW, No Forced AirC irculatio n ..................................................................................................

..36Table 6-2 Maximum Temperatures of CCNPP-FC TC for Accident Conditions

............

37Table 7-1 Maximum Temperatures of CCNPP-FC TC @ 29.6 kW, NO Forced AirC irculatio n ..................................................................................................

..4 8Table 7-2 Maximum Temperatures of CCNPP-FC TC for Accident Conditions

............

49Table 8-1 List of G eom etry Files ....................................................................................

50Table 8-2 Summary of ANSYS Runs .............................................................................

51Table 8-3 Associated Files and Macros ........................................................................

52Table B-1 Thermal Expansion Coefficients

....................................................................

56Table B-2 Density of Lead .............................................................................................

56Table D-1 Effective Density and Specific Heat [13] ......................................................

61Table D-2 Sensitivity of Maximum Temperatures to Effective Density and SpecificH e a t ...................................................................................................................

6 2Table E-1 Comparison of Solar Heat Load between 10 CFR 71.71 vs Design BasisValues for C C N PP-FC TC ............................................................................

63Table E-2 Solar Heat Flux Applied in the Sensitivity Analysis

........................................

64Table E-3 Sensitivity of Maximum Temperatures of Fuel Cladding, TC and DSCComponents to Solar Heat Load Boundary Conditions

................................

65LIST OF FIGURESPageFigure 5-1 Location of 32PHB DSC within CCNPP-FC TC .............................................

24Figure 5-2 Finite Element Model of CCNPP-FC TC with 32PHB DSC ..........................

25Figure 5-3 CCNPP-FC TC Finite Element Model, Components

.....................................

26 Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 5 of 65Figure 5-4Figure 5-5Figure 5-6Figure 5-7Figure 6-1Figure 6-2Figure 6-3Figure 6-4Figure 6-5Figure 6-6Figure 6-7Figure 6-8Figure 6-9Figure 6-10Gaps in CCNPP-FC TC M odel ......................................................................

27CCNPP-FC TC Finite Element Model, Cross Section ..................................

28Typical Decay Heat and Insolance Boundary Conditions

.............................

29Typical Convection and Radiation Boundary Conditions

..............................

30TC Temperature Distribution

-Vertical Loading Transient, t = 20 hr @29.6 kW, No Insolation, 1000F Ambient (load case # 5) ...............................

38DSC Shell Temperature Distribution

-Vertical Loading Transient, t = 20 hr@ 29.6 kW, No Insolation, 100°F Ambient (load case # 5) ..........................

39TC Temperature Distribution

-Off-Normal Hot Transient, t = 20 hr @29.6 kW, 127 Btu/hr-ft2 Insolation, 1040F Ambient (load case # 6) ...............

40DSC Shell Temperature Distribution

-Off-Normal Hot Transient, t = 20 hr@ 29.6 kW, 127 Btu/hr-ft2 Insolation, 1040F Ambient (load case # 6) ...........

41DSC Temperature Distribution

-Fire Accident, t = 15 min. @ 29.6 kW,1040F Am bient (load case # 7) ......................................................................

42TC Temperature Distribution

-Fire Accident, t = 15 min. @ 29.6 kW,1040F Am bient (load case # 7) ......................................................................

43TC Temperature Distribution

-Post-Fire

Accident, Steady State @ 29.62 okW , 127 Btu/hr-ft2, 1040F Ambient (load case # 7) ........................................

44DSC Shell Temperature Distribution

-Post-Fire

Accident, Steady State@ 29.6 kW, 127 Btu/hr-ft2, 1040F Ambient (load case # 7) ..........................

45Temperature History for Fire and Post-Fire Conditions

@ 29.6 kW, 1040FA m bient (load case # 7) ...............................................................................

46Bulk Average Temperature History of NS-3 in TC for Fire'and Post-Fire Conditions

@ 29.6 kW, 1040F Ambient (load case # 7) ...............................

47 Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 6of651.0 PURPOSEThis calculation determines the maximum component temperatures of the Calvert CliffNuclear Power Plant Onsite Transfer Cask (CCNPP-FC TC) loaded with 32PHB DSC at29.6 kW without forced convection.

It also establishes the maximum time limits fortransfer operations of a 32PHB DSC with 29.6 kW heat load in CCNPP-FC TC beforeinitiation of a corrective action such as forced air circulation or refilling the.TC/DSC annulus with clean demineralized water.The CCNPP-FC TC model provides the 32PHB DSC shell temperature distributions for32PHB DSC/Basket model to be evaluated in Reference

[13].

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 7 of 6

52.0 REFERENCES

1 U.S. Code of Federal Regulations, Part 71, Title 10, "Packaging and Transportation ofRadioactive Material".

2 U.S. Code of Federal Regulations, Part 72, Title 10, "Licensing Requirements for theIndependent Storage of Spent Nuclear Fuel and High-Level Radioactive Waste".3 Calvert Cliffs Independent Spent Fuel Storage Installation UPDATED SAFETYANALYSIS REPORT, Rev.17.4 Rohsenow,

Hartnett, Cho, "Handbook of Heat Transfer",

3rd Edition, 1998.5 Rohsenow,

Hartnett, Ganic, "Handbook of Heat Transfer Fundamentals",

2rd Edition,1985.6 ASME Boiler and Pressure Vessel Code,Section II, Part D, "Material Properties",

1998 with 1999 Addenda.7 ASME Boiler and Pressure Vessel Code,Section II, Part D, "Material Properties",

1992.8 Perry & Chilton, Chemical Engineers

Handbook, 5th Edition, 1973.9 American Institute of Steel Construction, "AISC Manual of Steel Construction,"

9thEdition.10 ANSYS computer code and On-Line User's Manuals, Version 10.0.11 Design Criteria

Document, "Design Criteria Document (DCD) for the NUHOMS32PHB System for Storage",

Transnuclear, Inc., NUH32PHB.0101 Rev. 4.12 Calculation, "NUHOMS 32P, Finite Element Model, Thermal Analysis",

Transnuclear, Inc., 1095-5 Rev. 0.13 Calculation, "Thermal Evaluation of NUHOMS 32PHB Canister for Storage andTransfer Conditions",

Transnuclear, Inc., NUH32PHB-0403, Rev.1.14 Calculation, "NUHOMS 32PHB Weight Calculation of DSC/TC System",Transnuclear, Inc., NUH32PHB-0201, Rev. 015 M. Greiner, S. Shin, B. Snyder and R.A. Wirtz, 1995, "Transportation PackageThermal and Shielding Response to a Regulatory Fire", Proc. 6th International HighLevel Radioactive Waste Management Conference, April 30-May 5, Las Vegas, NV,pp. 538-541.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 8of6516 Siegel, Howell, "Thermal Radiation Heat Transfer",

4th Edition, 2002.17 GESC, NAC International, Atlanta Corporate Headquarters, 655 Engineering Drive,Norcross, Georgia (Engineering Report # NS3-020, Effects of 1300°F on Unfilled NS-3, while Bisco Products, Inc., 11/84).18 Gregory, et al., "Thermal Measurements in a Series of Long Pool Fires", SANDIAReport, SAND 85-0196, TTC-0659, 1987.19 Weast, Astle, "CRC Handbook of Chemistry and Physics",

61st Edition, 1980-1981.

20 Calculation, "NUHOMS 32P -Transfer Cask Structural Analysis",

Transnuclear, Inc.,1095-35, Rev. 2.21 Calculation, "Reconciliation for Transfer Cask CCNPP-FC Structural Evaluation,"

Transnuclear, Inc., NUH32PHB-0211, Rev. 1.22 U.S.NRC, "Standard Review Plan for Spent Fuel Dry Storage Systems at a GeneralLicense Facility,"

NUREG 1536, Rev. 1.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 9 of 653.0 ASSUMPTIONS AND CONSERVATISM The following assumptions and conservatism are considered in the calculation.

3.1 CCNPP-FC TC ModelThe 32PHB DSC is located inside the CCNPP-FC TC such that a 0.5" gap exists betweenthe DSC and the bottom cover plate of the TC and 0.75" gap exists between the DSC andthe top cover plate of the TC. This reduces the axial heat transfer and maximizes the DSCshell temperature, which in turn result in higher fuel cladding temperature.

The decay heat load is simulated by heat generation distributed uniformly over the basketlength of 158" on the homogenized region. The basket is centered axially in the 32PHB DSC.A uniform gap of 0.375" is considered between the basket and the top/bottom ends of the32PHB DSC. This assumption reduces the axial heat transfer and maximizes the DSC shelltemperature, which in turn results in higher fuel cladding temperature.

For the transfer operations in horizontal orientation, the lower halves of the CCNPP-FC TCcylindrical surfaces are not exposed to insolance.

No solar heat flux is considered over thesesurfaces.

To remove any uncertainty about the solar impact on the vertical

surfaces, theentire surface areas of vertical surfaces are considered for application of the solar heat flux.During the transfer operation in vertical orientation, the DSC is assumed to be centeredwithin the transfer cask and heat transfer through the slide rails is neglected.

Further the topand bottom TC are modeled as adiabatic surfaces with only the outer shell surfacedissipating heat to the ambient.No convection is considered within the cask cavity for conservatism.

The grapple ring is not modeled in the current analysis; it is conservatively replaced with air.Radiation heat exchange is considered between the 32PHB DSC and the TC inner shell byusing the AUX12 processor with SHELL57 elements used to compute the form factors.The following gaps are considered in the CCNPP-FC transfer cask model:a) 0.0452" radial gap between the gamma shield and the structural shell.b) 0.06" axial gap between the top cover plate and the top flangec) 0.025" radial gap between the top cover plate and the top flanged) 0.75" radial gap between the bottom cover plate and the bottom end platee) 0.0625" axial gap between the various end plates in the DSC.No gap is considered between the neutron shield and the adjacent shells, since the neutronshield (NS-3) is poured in a controlled manner to avoid air pockets (See 4.7.3.3 of [3]).The radial gap "a" of 0.0452" between the gamma shield and structural shell is justified inAPPENDIX B.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 10 of 65Gaps "b" and "c" between the top cover plate and the top flange account for the thermalresistance between bolted components.

The radial gap "d" of 0.75" between the bottom cover plate and bottom end plate is largerthan the nominal gap. This is conservative since the hot gaps at thermal equilibrium would besmaller.The axial gaps "e" of 0.0625" between the DSC end plates maximizes the radial heat transferthrough DSC shell toward the TC to bound the maximum component temperatures conservatively.

For the fire accident conditions the gaps from "a" to "d" are replaced with the adjacentmaterials to allow heat input into the cask from the fire. The gaps are restored for the post-fire conditions.

3.2 32PHB DSC ModelThe assumptions and conservatism considered for 32PHB DSC model are the same asthose described in [13], Section 3.0, except those noted below.During loading operations, the water level in cask/DSC annulus is maintained 12" below theDSC top and is open to atmospheric pressure until the DSC is sealed. The water in theannulus will be observed and replenish as described in [3], Section 5.1.1.3.

These operational requirements prevent annulus water from approaching boiling temperature and assure thatthe DSC shell temperature doesn't exceed the boiling temperature of water.Therefore, a conservative DSC shell temperature of the 212°F is used for establishing theinitial conditions in the CCNPP-FC TC when the TC is in the vertical orientation and theDSC/TC annulus is filled with water. See APPENDIX C for justification of DSC shelltemperature.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 11 of 654.0 DESIGN INPUT4.1 Design Load CasesThe following design cases in Table 4-1 are analyzed in this calculation to determine thethermal performance of CCNPP-FC TC with 32PHB DSC at 29.6 kW and without forcedconvection (FC). The load cases are based on requirements in [11].Table 4-1 Design Load Cases for 32PHB DSC in CCNPP-FC TC without FCAmbientCase Operation Condition Description Notes Temperature Insolation Airflow[°F] [Btu/hr-ft 2] [cfm]1 Normal Normal Hot (3) 104 82 02 Normal Normal Cold (3) -8 0 03 Off-Normal Off-Normal Hot (3) 104 127 04 Off-Normal Off-Normal Cold (3) -8 0 05 Normal Vertical Operations, Transient (1) 100 0 06 Off-Normal Off-Normal Hot, Transient (1) 104 127 07 Accident Fire Accident (2) 104/1475/104 127 0Notes:1) Initial steady-state conditions with 212°F water assumed in the DSC/TC annulus.

At time t=0, the water isdrained, no forced air circulation is available, and the system begins to heat up.2) 15 Minute Fire Transient.

1OCFR71.

73 [1] fire criteria used for fire properties with a fire emissivity of 1.0.Initial temperatures taken from transient results at 20 hours2.314815e-4 days <br />0.00556 hours <br />3.306878e-5 weeks <br />7.61e-6 months <br /> in load case # 6 (i.e. the time limit for transferoperations without forced air circulation).

Post-fire condition assumes the decomposition of the neutronshield with no forced convection available.

3) Load cases # 1, 2, 3 and 4 are bounded by the Load Case # 6 (See Section 6.0 for justification).

4.2 Major Dimensions in the CCNPP-FC TC ModelMajor dimension of 32PHB DSC used in the CCNPP-FC TC model are listed in Table 4-2below.All other dimensions are based on nominal dimensions of CCNPP-FC transfer cask drawingslisted in DWG NUH32PHB-30-1

1.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 12of65Table 4-2Major Dimension of 32PHB DSC in CCNPP-FC TC model [14]DSC Component Length[in]Bottom End PlatesBottom Lead Casing Plate 0.50Bottom Lead Shielding 4.25Bottom Cover Plate 1.75Top End PlatesLead Plug Top Casing Plate 0.75Top Lead Shielding 4.00Top Inner Cover Plate 1.50Outer Top Cover Plate 1.25Cavity Length 158.75(1)

DSC Length 172.75(w/o grapple)Basket height 158.00Note 1: 158.63"is the minimum length for DSC the cavity as shown in [14]. However, the nominallength of 158.75" used in this calculation

[Nominal Cavity Length = DSC Length (172.75")

-Totalthickness of the top end plates (7.5") and bottom end (6.5")].4.3 Thermal Properties of Materials Materials used in CCNPP-FC TC model are listed in Table 4-3. Thermal properties used inCCNPP-FC TC model are listed in Table 4-4 through Table 4-13 for reference.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 13of65Table 4-3List of Materials in the CCNPP-FC TC ModelComponent Mat # in ANSYS Model MaterialTransfer Cask Properties Bottom Cover Plate (1" thick) 101 SA240 Type 304Bottom End Plate (0.75" thick) 102 SA240 Type 304Bottom Support Ring 103 SA182 F304NBottom Cover NS-3 (3.5" thick) 104 NS-3Plate for Bottom Cover (0.5" thick) 105 SA240 Type 304Bottom Castable NS-3 (3.63" thick) 106 NS-3Bottom Cover Plate (2" Thick) 107 SA240 Type 304Ram Access Machined Ring 108 SA182 Type F304NPlate for Top Cover (0.25" thick) 109 SA240 Type 304Top Cover NS-3 (3" thick) 110 NS-3Top Cover Plate (3" thick) 111 SA240 Type 304Inner Shell (0.75" thick) 112 SA240 Type 304Lead Shielding (Gamma Shield, 4" 113 ASTM B29thick) 113__STMB29 Structural Shell (1.5" & 2" thick) 114 SA516 GR70Top Flange 115 SA182 Type F304NNeutron Shield Panel (0.25" thick) 116 SA240 Type 304NSP Support Angle (0.25" thick) 117 SA240 Type 304Radial Neutron Shield (4" thick) 118 NS-3Rails (0.12" thick) 119 Nitronic 60 (Effective Properties used.See Section 5.3)DSC Properties DSC Shell 301 SA240 Type 304DSC Bottom Shield Plug Assembly 302 Effective Properties used, See Section5.4.2DSC Top Shield Plug Assembly 303 Effective Properties used, See Section+ Top Outer Cover Plate 5.4.1DSC Helium Gap 304 HeliumDSC Basket 305 Homogenized Region, Effective Properties

[See Table 4-10]Gaps in ModelGap Between Bottom Cover Plate 201 Airand Bottom End PlateGaps in Grapple Region 202 AirGap between the DSC and the TCbottom cover plate/TC top cover plate 203 Airand also between the Top Flangeand TC Top cover plateGap between the DSCITC Annulus 206 AirGap between Gamma Shield and 205 AirStructural Shell I I Calculation No.: NUH32PHB-0402 Revision No.: 1Page: 14 of 65Table 4-4Stainless Steel, SA 240, Type 304 / SA 182 Type F304N [6-8]Temp P k Cp(OF) (Ib/in3) (Btu/hr-in-°F)

(Btu/Ib-°F) 70 0.717 0.114100 0.725 0.114200 0.775 0.119300 0.817 0.122400 0.867 0.126500 0.290 0.908 0.128600 0.942 0.130700 0.983 0.132800 1.017 0.132900 1.058 0.1341,000 1.100 0.136rable 4-5 Carbon Steel, SA 516, Gr.70 [7, 9Temp P 3 k Cp(OF) (Ib/in) (Btu/hr-in-°F)

(Btu/Ib-°F) 70 1.967 0.106100 1.992 0.110200 2.033 0.118300 2.033 0.122400 2.017 0.128500 0.284 1.975 0.133600 1.925 0.136700 1.867 0.143800 1.808 0.148900 1.742 0.1551,000 1.667 0.164ITable 4-6Gamma Shield, ASTM B29 Lead [5]Temp P 3 K Cp(OF) (Ib/in) (Btu/hr-in-°F)

(Btu/lb-°F)

-279 0.416 1.912 0.028-189 0.414 1.825 0.029-99 0.413 1.767 0.030-9 0.411 1.733 0.03081 0.409 1.700 0.031261 0.406 1.637 0.032441 0.402 1.579 0.033621 0.398 1.512 0.034 Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 15of65Table 4-7Castable Neutron Shield, NS-3 [12, 15]Operation Condition k C" DensityNormal & Fire Accident (Btu-in/hr-in

-OF) (Btu/Ibm-'F)

-"(lb/in3) 0.0407 0.145 0.0637k C DensityPost-Fire Accident (Btu-in/hr'in

'-°F) (Btu/lbm-'F)

(lb/in')_' 0.0114 0.145 0.0605 Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 16 of 65Table 4-8Air Thermal Properties

[4]Temperature Thermal conductivity Temperature Thermal conductivity (K) (W/m-K) (OF) (atu/hr-in-°F) 200 0.01822 -100 0.0009250 0.02228 -10 0.0011300 0.02607 80 0.0013400 0.03304 260 0.0016500 0.03948 '440 0.0019600 0.04557 620 0.0022800 0.05698 980 0.00271000 0.06721 1340 0.0032The above data are calculated based on the following polynomial function from [4].k = -C T' for conductivity in(W/m-K) and T in (K)For 250 < T < 1050 KCo -2.2765010E-03 C1 1.2598485E-04 C2 -1.4815235E-07 C3 1.7355064E-10 C4 -1.0666570E-13 C5 2.4766304E-17 Specific heat, viscosity, density and Prandtl number of air are used to calculate heattransfer coefficients in APPENDIX A based on the following data from [4].cp =iAj T'for specific heat in (kJ/kg-K) and T in (K)________________For 250< T < 1050 KAO 0.1 03409E+1Al -0.2848870E-3 A2 0.7816818E-6 A3 -0.4970786E-9 A4 0.1077024E-12 for viscosity (N-s/m2)xl06 and T in (K)IFor 250 < T < 600 KB0 -9.8601E-1 B1 9.080125E-2 B2 -1.17635575E-4 B3 1.2349703E-7 B4 -5.7971299E-11 For600 < T < 1050 KB0 4.8856745 B1 5.43232E-2 B2 -2.4261775E-5 B3 7.9306E-9 B4 -1.10398E-12 p = P / RT for density (kg/m3) with P=1 01.3 kPa; R = 0.287040 kJ/kg-K; T = air temp in (K)Pr =cp ýi/kPrandtl number Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 17 of 65Table 4-9Helium Thermal Conductivity

[4]Temperature Thermal conductivity Temperature Thermal conductivity (K) (W/m-K) (OF) (Btu/hr-in-°F) 300 0.1499 80 0.0072400 0.1795 260 0.0086500 0.2115 440 0.0102600 0.2466 620 0.0119800 0.3073 980 0.01481000 0.3622 1340 0.01741050 0.3757 1430 0.0181Ine aDove oaaa are calculated based onfrom [4]k = -Ci T' for conductivity in (W/the following polynomial functionIIrn-K) and T in (K)For_300 < T < 500 K for_500<

T < 1050 KCO -7.761491E-03 CO -9.0656E-02 Cl 8.66192033E-04 Cl 9.37593087E-04 C2 -1.5559338E-06 C2 -9.13347535E-07 C3 1.40150565E-09 C3 5.55037072E-10 C4 O.OE+00 C4 -1.26457196E-13 Table 4-10Thermal Properties of Homogenized Basket(')

[13]Temp kbasket rad Temp kbasket, axd Temp Co erf Pef(OF) (Btu/hr-in-°F)

(OF) (Btu/hr-in-OF)

(OF) (atu/lbm-°F)

(lb/in')3150.1511001.9946700.095403 0.160 200 2.0393 100 0.096492 0.169 300 2.0760 200 0.098581 0.179 400 2.1055 300 0.099672 0.189 500 2.1160 400 0.100763 0.199 600 2.1228 500 0.101855 0.209 700 2.1297 600 0.101949 0.218 800 2.1355 700 0.1011045 0.224 900 2.1418 800 0.1011143 0.227 1000 2.1474 900 0.1020.13110000.102Note 1: See Appendix D for justification of effective density and specific heat.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 18of65Table 4-11Effective Conductivity of Top Shield(See Section 5.4.1 for Justification)

Plug and Top Cover PlateTemp kradial k axial Cpeff Pef3(OF) (Btu/hr-in-°F)

(Btu/hr-in-°F)

(Btu/Ibm-°F)

(lb/in3)70 1.243 0.048 0.062100 1.241 0.051 0.062200 1.246 0.058 0.064300 1.247 0.064 0.065400 1.268"' 0.071 0.067500 1.254 0.077 0.068 0.352600 1.250 0.083 0.068700 1.249 0.088 0.069800 1.245 0.094 0.069900 1.244 0.099 0.0701,000 1.244 0.104 0.071Note: (1) 1.255 Btu/hr-in-0F is conservatively used in the analysisTable 4-12Effective Conductivity of Bottom Shield Plug(See Section 5.4.2 for Justification)

Temp kradial kaxial Cpeff Pe3(OF) (Btu/hr-in-F)

(Btu/hr-in-F)

(Btu/Ibm-°F)

(Ib/in)70 1.362 0.062 0.053100 1.358 0.065 0.053200 1.352 0.074 0.054300 1.345 0.082 0.055400 1.358 0.090 0.056500 1.332 0.098 0.057 0.367600 1.320 0.105 0.057700 1.309 0.112 0.058800 1.297 0.119 0.058900 1.286 0.126 0.0581,000 1.276 0.132 0.059 Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 19 of 65Table 4-13Effective Conductivity of Slide Rail(See Section 5.3 for Justification) trail = 0.12 inh contact = 2.7 Btu/hr-in 2-OFTemp k SS304 k eff(F) (Btu/hr-in-°F)

(Btu/hr-in-°F) 70 0.717 0.223100 0.725 0.224200 0.775 0.228300 0.817 0.232400 0.867 0.236500 0.908 0.239600 0.942 0.241700 0.983 0.244800 1.017 0.246900 1.058 0.2481000 1.100 0.2504.4 Surface Properties of Materials The emissivity value of 0.587 is considered for both the DSC shell (stainless steel) and thetransfer cask inner shell (stainless steel) in calculation of thermal radiation exchangebetween these shells [4].It is assumed that the absorptivity and the emissivity of stainless steel are equal. Solarabsorptivity and emissivity of 0.587 are used for the TC outer surfaces

[4].After fire, the cask outer surfaces will be partially covered in soot. Based on [16], emissivity and solar absorptivity of soot are 0.95. The fire accident thermal analysis conservatively assumes a solar absorptivity of 1.0 and an emissivity of 0.9 for the post fire, cool-down period.4.5 Design CriteriaThe design criteria for the TC are established by temperature limits of its temperature sensitive components.

These are the temperature of the lead in the gamma shield and thetemperature of the NS-3 solid neutron shielding material.

The melting point of ASTM B29 lead used in the gamma shield is approximately 620OF [8].For design purposes of this application, the long-term, bulk average temperature of the NS-3material is set to 280 IF [3] or less, and short-term limits for accident conditions should be1,300 OF or less [17].

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 20 of 65The design criteria and evaluation of 32PHB DSC basket for the various load cases shown inTable 4-1 are presented in Reference

[13].

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 21 of 655.0 METHODOLOGY 5.1 CCNPP-FC TC ModelA half-symmetric, three-dimensional finite element model of CCNPP-FC transfer cask (TC) isdeveloped using ANSYS Version 10.0 [10] to provide the DSC shell temperature profile for32PHB DSC model and to determine the maximum component temperatures of the CCNPP-FC TC for various load cases described in Table 4-1.The model contains the cask shells, cask bottom plate, cask lid, DSC shell, and DSC endplates with a homogenized basket. The 32PHB DSC dimensions correspond to nominaldimensions listed in Table 4-2.SOLID70 elements are used to model the components including the gaseous gaps. Surfaceelements SURF1 52 are used for applying the insolation boundary conditions.

Radiation alongthe gap between DSC and TC inner shell is modeled using AUX12 processor with SHELL57elements used to compute the form factors.Decay heat load is applied as a uniform volumetric heat generated throughout thehomogenized region of the basket. The volumetric heat generation rate is calculated asQ;r(D,/2)2 Lbq' = Volumetric Heat Generation Rate (Btu/hr-in 3)Q = decay heat load (Btu/hr)

(to convert from kW multiply by 3412.3)Di = DSC inner Diameter (in)Lb = Basket length (in)The applied decay heat value in the model is listed in Table 5-1Table 5-1 Decay Heat LoadDSC Type Heat Load Heat Load Di Lb Decay heat Load(kW) (Btu/hr)

(in) (in) (Btu/hr-in 3)32PHB 29.6 101004 66 158 0.1869For load cases with insolance, the insolance is applied as a heat flux over the TC outersurfaces using average insolence values listed in Table 4-1. The insolance values aremultiplied by the surface absorptivity factor to calculate the solar heat flux. The solar heat fluxvalues used in CCNPP-FC TC model are summarized in Table 5-2.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 22 of 65Table 5-2 Solar Heat FluxOperating Condition Solar Heat Flux Solar Total solar heat flux(Btu/hr-ft

2) Absorptivity (1) (Btu/hr-in 2)Normal 82 0.587 (2) 0.334Off-Normal/Accident 127 0.587 (2) 0.518Note (1): See Section 4.4 for surface properties.

Note (2): Solar absorptivity of stainless steel is taken equal to its emissivity.

Convection and radiation heat transfer from the cask outer surfaces are combined togetheras total heat transfer coefficients.

The total heat transfer coefficients are calculated using freeconvection correlations from Rohsenow Handbook

[4] and are incorporated in the modelusing ANSYS macros. These correlations are described in APPENDIX A. The ANSYSmacros used in this calculation are listed in Section 8.0.During transfer when the cask in a horizontal orientation, the DSC shell rests on two sliderails in the TC. These rails are flat stainless steel plates welded to the inner shell of the TC.The thickness of the slide rail is 0.12".The angle between the lower rail and the vertical plane is 18.5 degree. Considering thisconfiguration shown in Figure 5-1, the distance between the centerline of DSC and centerline of the cask are calculated as follows.R2 2 R+ X2 -2 R x Cos(a)WithR, = Di, TC/2 -trailR2= Do, DSc / 2a = 18.50x = Distance between the DSC and TC centerlines (See Table 5-3)D, TC = Inner diameter of TC (See Table 5-3)Do, Dec= DSC outer diameter (See Table 5-3)trail = cask slide rail thickness

= 0.12"The calculated value for x is listed in Table 5-3. In the ANSYS model, the DSC is shifteddown by the amount of x in the Cartesian y-direction within the TC cavity.Table 5-3 Distance between 32PHB DSC and TC Centerline DSC Type Di,Tc Do,DSC R1 R2 a x(in) (in) (in) (in) (degree)

(in)32PHB 68 67.25 33.88 33.625 18.5 0.27 Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 23 of 65The material properties used in the CCNPP-FC TC model are listed in Section 4.0.The geometry of the TC model and its mesh density are shown in Figure 5-2 to Figure 5-5.Typical boundary conditions for TC model are shown in Figure 5-6 through Figure 5-7.5.2 Fire AccidentFor the fire accident

analysis, a diesel fuel pool of 190" in diameter, which is the approximate length of the TC, is conservatively assumed to engulf the entire cask. A maximum fuel spill of100 gallons of diesel fuel which is the maximum capacity of both fuel tanks within the towvehicle is considered in Section 3.3.6 of CCNPP ISFSI USAR [3]. For this postulated fireaccident with a conservative volume of 200 gallons of diesel fuel spill, the thickness of thefuel pool would be 1.63". This pool is assumed to burn at a minimum burning rate of 0.15in/min [18]. The 1.63" thick fuel pool would burn for 11 minutes.

For conservatism a 15minute fire duration is considered in this analysis.

To determine the maximum temperature of TC and DSC shell during the fire accident, atransient fire analysis is performed for duration of 15 minutes using the criteria described in10CFR71, part 73 [1]. Based on the requirements in 10 CFR 71, part 73 [1], a firetemperature of 1475 OF and a conservative fire emissivity of 1.0 are considered for the fireconditions.

Surface emissivity of 0.8 is considered for the packaging surfaces exposed to firebased on 10 CFR 71, part 73 [1]. A bounding forced convection coefficient of 4.5 Btu/hr-ft 2-OFis considered during burning period based on data from reference

[18]. The initial conditions for the fire analysis are obtained from the transient results at 20 hours2.314815e-4 days <br />0.00556 hours <br />3.306878e-5 weeks <br />7.61e-6 months <br /> in load case # 6 (SeeTable 4-1) (i.e. the time limit for transfer operations without forced air circulation).

From Reference

[17], when NS-3 material was heated in a furnace to a temperature of1300°F +/- 100°F (50 minutes to get to 13000F) for a period of one hour, the weight loss fromNS-3 was 41 percent.

A white smoke started to come out of the furnace at a temperature of600°F and continued for the duration of the test. At the end of the test, the NS-3 was solid(consisting of inorganic constituents),

it did not burn, and was brittle with no mechanical strength.

The thermal properties of the NS-3 for the post-fire conditions are obtained fromRef [15] and listed in Table 4-7.Transient runs are performed for 48 hours5.555556e-4 days <br />0.0133 hours <br />7.936508e-5 weeks <br />1.8264e-5 months <br /> after the fire. The results of the transient runsdiscussed in Section 6.0 show that the maximum temperatures of cask components exceptfor the components on the exterior surfaces of the TC and NS-3 are increasing during post-fire conditions so that the maximum cask component temperatures obtained for steady-state post-fire conditions bound the maximum temperatures of the TC and DSC for fire accidentconditions.

The DSC shell temperature profiles from steady state runs will be used to determine themaximum basket component temperatures including the maximum fuel cladding temperature in a separate calculation

[13].

Calculation No.: NUH32PHB-0402 Revision No.: 1Page: 24 of 65TC Cta= 18.50R0 = Di, TC /2 -trailR2 = Do. DSC / 2R1DSC CtSlide RailFigure 5-1Location of 32PHB DSC within CCNPP-FC TC Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 25 of 65Gamma ShieldCavity GapNeutron ShieldIStructural Shell/TC Bottom NS-3 DSC End TC Top Cover TC Top NS-3PlatesFigure 5-2Finite Element Model of CCNPP-FC TC with 32PHB DSC Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 26 of 65Gamma ShieldCask Outer ShellRam Cask LidClosurePlateCask Inner LinerDSC Bottom Plates\ tFigure 5-3CCNPP-FC TC Finite Element Model, Components Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 27 of 650.0452" radial gapbetween structural shell and gammashield0.75" Radial Air Gap/0.375" axial gapbetween the basketand DSC end plates0.06" Axial AirGap betweenthe top flangeand TC top lidAir in the GrappleRegion0.5" Axial AirGap betweenthe DSC andTC bottom0.75" Axial Air 0.025" radialGap between Air Gapthe DSC and between theTC top lid top flange andTC top lidFigure 5-4 Gaps in CCNPP-FC TC Model A Calculation No.: NUH32PHB-0402 Calculation Revision No.: 1AREVA Page: 28 of 65Structural Shell/DS6r I-'44AnnulusDSC ShellGamma ShieldNeutron Shield RibsMINeutron ShieldInner LinerHorizontal TC (DSC is offset)CCNPP-FC TC Finite Element Model, Cross SectionFigure 5-5 Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 29 of 65ANELEMENTSHGEN RATESQMIN=0QMAX=. 1868540.020762.041523.062285.083046-.103808m .12457L-- .145331-.166093I .186854iliedonUniform Volumetric Heat Generation appthroughout Homogenized Basket RegiInsolance Boundary Conditions Figure 6-6Typical Decay Heat and Insolance Boundary Conditions Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 30 of 65ANSYS 10.OAIOCT 5 200913:27:38ELEMENTSPowerGraphics EFACET=1MAT NUMXV =.630637YV =.250458zv =.734553*DIST=88.

614*XF =23.853*YF =-16.313*ZF =97.502A-ZS=-3.

005Z-EBUFFER EDGECONV-HCOV m -5*053-504-503-502-501Figure 5-7Typical Convection and Radiation Boundary Conditions Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 31 of 655.3 Effective Conductivity of Slide RailsWhen the TC is in the horizontal orientation, the DSC is supported by the two rails depictedin DWG # BGE-01-3002.

Given the weight of a loaded DSC (i.e., > 100,000 Ibs) and thesurface area of the rails (i.e., 3-inch wide x 167.50-inches long), the contact pressurebetween a loaded DSC and the rail is in excess of 99 lbs/in2 (assuming contact with tworails). The thermal resistance between the DSC and the canister rails is assumed to beapproximately 2.7 Btu/hr-in 2-OF [per Curve 11, page 4-19, Ref. 5].The effective conductivity for the rails is calculated based on the following equation and isshown in Table 4-13:keff= ritrail 1kra,1 hres tan cewhere:trail = Thickness of the Rail = 0.12"krail = Conductivity of NITRONIC 60 Rails(Assumed to be SA240 Type 304, See Table 4-4)hresistance

= Contact Resistance

= 2.7 Btu/hr-in 2-OF5.4 Effective Thermal Properties of DSC End PlatesThe various end plates at the top and bottom of the DSC are modeled as a homogenized region with effective conductivity, density and specific heat.5.4.1 Top Shield Plug Assembly and Top Cover PlateThe effective properties for the end plates at the top of the DSC are calculated based on thefollowing dimensions Table 5-4 Thickness and Weights of the Top End AssemblySee Table 1 of Reference

[14]Component Thickness Volume Weight Material[in] [in3] [Ib]Inner Top Cover Plate 1.5 5,107 1,461 SA240 Type 304Top Shield Plug 4 13,208 5,429(2)

ASTM B29Top Casing for Lead') 0.75 2,477 708(2) SA240 Type 304Outer Top Cover Plate 1.25 4,245 1,214 SA240 Type 304Note (1): The lead plug side casing plate is neglected.

Note (2): The weight of the Top Shield Plug and Top Casing for Lead are 5428 lbs and 709 Ibs, respectively asshown in Table 1 of Reference

[14]. The effect on the effective properties due to these changes is negligible.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 32 of 65Effective Thermal Conductivity Axial air gaps of 0.0625" are considered between each plate shown in the above table.These gaps account for contact resistance and fabrication imperfections between thesecomponents and adjacent plates.The various end plates along with the 0.0625" axial gaps between them built up serialthermal resistances along the axial direction.

The effective conductivity through the serialplates is:atpte t,,c' +tsp +tI +ct!,p +(n* tK )keff.arial

-tplate titu ttsp to tticp *tgapE p t + + + t +kpate khi p ktsp k,.l k,,Cp a ..gapwhere:ttcp, ttsp, ttcl, totcp, tgap = thickness of inner top cover plate, top shield plug, top casing for lead,outer top cover plate and air gap, respectively (See Table 5-4).kitcp ktsp, ktckotcp, kair = Thermal conductivity of inner top cover plate, top shield plug, topcasing for lead, outer top cover plate and air gaps, respectively (See Table 5-4 for materials and Section 4.3 for thermal conductivities).

The various end plates built up parallel thermal resistances along the radial direction.

Theeffective conductivity through the parallel plates is:keg ff.a, X (kplae*tpte)

-k,,tp

• t,,'p + kp

• t,,p + k,c,

• tc, + ko,,p

• t,,pkEff~ri tplate tcsps+ ptU + tl atpwhere:titcp, ttsp, ttcl, totcp = thickness of inner top cover plate, top shield plug, top casing for lead andouter top cover plate, respectively (See Table 5-4).kitcp, ktsp, ktc, kotcp = Thermal conductivity of inner top cover plate, top shield plug, top casingfor lead and outer top cover plate, respectively (See Table 5-4 for materials and Section 4.3for thermal conductivities).

The effective radial and axial thermal conductivities for the top shield plug and top cover plateare shown in Table 4-11.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 33 of 65Effective DensityThe effective density of the end plates is calculated as follows:Ip p'a,e

• Vpia. ie,,cp

• VCi +

• VP + p,..

• vKC, +

• Vo..peff VTo.o, V,,CP +v +,, ++/-V" +Vo,where:titcp,, ttc, totcp = thickness of inner top cover plate, top shield plug, top casing for lead andouter top cover plate, respectively (See Table 5-4).Vitcp,,,

Vt, Vote = Volume of inner top cover plate, top shield plug, top casing for lead andouter top cover plate, respectively (See Table 5-4).Effective Specific HeatThe effective specific heat for the end plates is calculated as follows:CPef= Wpotw

• Cpp,t= W_ tcp

• Cpit1p + WtsP

• Cpt,p + WMc,

• Cptc, + Wotcp

• Cp0cpeWTotW, W,4p + Wt.V + Wto, + where:Cptcp,, Cpt, Cptc, Cpotcp = Specific Heat of inner top cover plate, top shield plug, top casing forlead and outer top cover plate, respectively (See Table 5-4 for materials and Section 4.3 forCp values).Witcp, Wtsp, Wtcl, Wotcp = Density of inner top cover plate, top shield plug, top casing for leadand outer top cover plate, respectively (See Table 5-4).A constant specific heat of 0.030 Btu/Ib-0F is used for lead in the calculation of effective specific heat. This is conservative since this decreases the heat capacity.

The effective density and specific heat for the top shield plug and top cover plate are shownin Table 4-11.5.4.2 Bottom Shield Plug AssemblyThe effective properties for the end plates at the bottom of the DSC are calculated based onthe methodology described in Section 5.4.1 and the following dimensions Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 34 of 65Table 5-5Thickness and Weights of the Bottom End AssemblySee Table 1 of Reference

[14]Component Thickness Volume Weight Material[in] [in3] ) [Ib]Inner Bottom Cover Plate 1.75" 6,216 1,778 SA240 Type 304Bottom Shield Plug 4.25" 14,650 6,021 ASTM B29Bottom Casing for Lead"' 0.5" 1,623 464 SA240 Type 304Note (1): The lead plug side casing plate is neglected.

The effective thermal properties for the bottom end plates of the 32PHB DSC are presented in Table 4-12.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 35 of 656.0 RESULTS AND DISCUSSION Due to the high decay heat load of 29.6 kW considered for the NUHOMS 32PHB system thetransfer operations under normal and off-normal steady state conditions listed in Table 4-1(load case # 1 to 4) are not permitted and operational time limits to complete the transferoperations are established based on the transient thermal analyses performed for normalvertical transfer conditions (load case # 5, Table 4-1) and off-normal hot horizontal transferconditions (load case # 6, Table 4-1). The time limit established for off-normal hot transferconditions bounds the time limits for normal hot/cold and off-normal hot/cold conditions.

For the vertical loading transient condition (load cases # 5), the transient begins at steadystate with 212°F water in the TC-DSC annulus and the cask is in vertical orientation (i.e. nocredit is taken for heat transferred through the rail). At time t= 0, the water in the cask isassumed to be drained, and the cask closure is completed.

The TC is assumed to be leftinside the fuel building in the vertical position.

For the off-normal hot transient condition (load case # 6), at time = 0, the cask is assumed tobe drained, and the cask closure is completed, TC is assumed to be rotated to a horizontal orientation and moved outdoors.

For practical

purposes, the time limits for vertical or horizontal transfer operations should beconsidered after sealing the DSC when the water in the TC/DSC annulus starts to be drainedcompletely.

The NUHOMS 32PHB system has a provision for forced convection to improve the thermalperformance of the system during horizontal transfer conditions and is to be used only as onepossible recovery mode if the operational time limits determined for load case # 6 in Table4-1 are exceeded.

The thermal performance of the NUHOMS 32PHB system with forced airconvection will be analyzed in a separate calculation.

The forced air convection is not reliedon for accident conditions.

Based on the transient thermal analyses a maximum duration of 20 hours2.314815e-4 days <br />0.00556 hours <br />3.306878e-5 weeks <br />7.61e-6 months <br /> is allowed for boththe vertical transfer operations (load case # 5) and the off-normal hot horizontal transferoperations (load case # 6). Table 6-1 summarizes the maximum temperatures for theCCNPP-FC TC components and shows that the maximum component temperatures arebelow the allowable limits for transfer duration of 20 hours2.314815e-4 days <br />0.00556 hours <br />3.306878e-5 weeks <br />7.61e-6 months <br />.Figure 6-1 and Figure 6-2 show the temperature distribution of the CCNPP-FC TC and32PHB DSC for vertical transient conditions.

Figure 6-3 and Figure 6-4 present the temperature profiles for the off-normal horizontal transfer condition at 20 hours2.314815e-4 days <br />0.00556 hours <br />3.306878e-5 weeks <br />7.61e-6 months <br /> for the CCNPP-FC TC and 32PHB DSC.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 36 of 65Table 6-1 Maximum Temperatures of CCNPP-FC TC @ 29.6 kW,No Forced Air Circulation Temperature

[OF]Component Vertical Hot Off-Normal Hot Max. Allowable Load Case # 5 Load Case # 6time = 20 hrMax. DSC Shell " 395 407Inner Shell 279 313Gamma Shield 277 308 620 [8]Structural Shell 242 263 ---Bulk Avg. Temp ofRadial Neutron Shield 201 214 280 [3]Bulk Avg. Temp ofTop Neutron ShieldBulk Avg. Temp ofBottom Neutron Shield 240 201Cask Lid 242 216 ---Cask Outer Shell 238 233 ---(1) The maximum DSC shell temperature is the temperature along the "DSC Shell" as shown in Figure 5-3 anddoes not include the top and bottom end plates.Figure 6-5 and Figure 6-6 show the temperature profiles of the DSC and TC at the end of 15minute fire. Figure 6-7 and Figure 6-8 show the temperature profiles for the steady statepost-fire conditions.

Table 6-2 presents the maximum component temperature at the end of15 minute fire, at 48 hours5.555556e-4 days <br />0.0133 hours <br />7.936508e-5 weeks <br />1.8264e-5 months <br /> into post-fire and for the steady state post-fire conditions.

Figure 6-9 shows the temperature history of the TC components, DSC Shell andHomogenized Basket during the fire and post-fire conditions.

As seen from the figure andTable 6-2, the TC component, the DSC shell and basket temperatures are increasing duringthe post-fire transient analysis and the maximum temperatures will be achieved under post-fire steady state conditions except for the components on the exterior surfaces of the TC andneutron shield.Figure 6-10 shows the bulk average temperature history of the NS-3 neutron shield in the TCduring and after the fire accident.

As seen from the Figure 6-10 the bulk averagetemperatures of the NS-3 components in the TC increase during the fire and their maximumtemperatures are attained at the end of the fire and are listed in Table 6-2.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 37 of 65Table 6-2Maximum Temperatures of CCNPP-FC TC for Accident Conditions Temperature

[°F]Fire Accident Post-Fire

@ 48 Hours Post-Fire Steady State Max. Allowable Component (15 Min. End of after FireFire)Max. DSC Shell (" 408 565 656Inner Shell 307 492 590 ---Gamma Shield 415 487 585 620 [8]Structural Shell 352 447 568 --Bulk Avg. Temp of 542 295 359 1300 [17]Radial Neutron ShieldBulk Avg. Temp of 640 231 258 1300 [17]Top Neutron ShieldBulkAvg.

Temp of 441 258 291 1300 [17]Bottom Neutron ShieldCask Lid 910 290 335 ---Cask Outer Shell 1321 332 398 ---(1) The maximum DSC shell temperature is the temperature along the "DSC Shell" as shown in Figure 5-3 anddoes not include the top and bottom end plates.The maximum thermal stresses for the TC components except for the bottom cover plate andthe ram access penetration ring occur during the hot ambient conditions as noted in Table4.1.2.1 of [20]. Further the maximum stresses for the bottom cover plate and ram accesspenetration ring during the cold ambient conditions are significantly below the allowable stress limits. Therefore, the temperature gradients determined for the load case # 6 (Table4-1, off-normal horizontal hot transfer conditions) are acceptable for the structural evaluation of thermal stresses for the CCNPP-FC TC with 32PHB DSC.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 38 of 65AN OCT 21 200918: 33: 36PLOT NO. 4NOEDL SOIUTIONTIME=20STM =162.269SM =278.741m 162.269m 15.21188.152201.093214.034-226.975239.917252.858265.799278.741OCMP-FC-TC with 32PHB, 29.6 kW -Vertical in Fuel Bldg Transient AN OCT 21 200918:33:34PKDT NO. 3NODAL SOIUTONTBF--20TEMPSMN =162.269SMK =278.741m162.269mm175.21188.152201. 093mm214.034 226.975[-7239.917 m 252.858m265.799278.741OCW-FC--TC with 32PMB, 29.6 kW -Vertical in Fuel Bldg Transient Figure 6-1 TC Temperature Distribution

-Vertical Loading Transient, t = 20 hr@ 29.6 kW, No Insolation, 100°F Ambient (load case # 5)

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 39 of 65AN OCT 21 200918: 33: 34PIwr NO. 2NODAL SOLUTIONTIME=20TEMPSMt =325.719SMX =440.551325.719338.478351.237363.996376.755389.514402.273415.033427.792440.551CtWP-FC-TC with 32PHB, 29.6 kW -Vertical in Fuel Bldg Transient AN OCT 21 200918: 33: 33PLT NO. 1NODAL SOLUIMONTDhE=205MN =325.719SK -=440.551 325. 719338.478351.237363.996376.755389.514-402.273415.033427.792440.551(flIF-FC-IC with 32PHB, 29.6 kW -Vertical in Fuel Bldg Transient Figure 6-2 DSC Shell Temperature Distribution

-Vertical Loading Transient, t = 20 hr@ 29.6 kW, No Insolation, 100IF Ambient (load case # 5)

Calculation No.: NUH32PHB-0402 Calculation Revision No.: 1AREVA Page: 40 of 65AN OCT 21 200918:28:23PLOT NO. 4NODAL SOITIONTIbE=20SMN =163.456SM3 =313.262163.456180.101196.746213. 391230.037246.682263.321279.972296.617313.262E'EP-FC-TC with 32PMB, 29.6 kW -Off-Normal Transfer Transient RunsAN OCT 21 200918:28:22PLOT NO. 3NODAL SOCLLIONTIME=20TEMPSMN =163.456SM =313.262163.456180.101196.746213.391230.037246.682-263.327279.972296.617313.262OMIP- TC-' with 32PHB, 29.6 kW -Off-Normal Transfer Transient PunsFigure 6-3 TC Temperature Distribution

-Off-Normal Hot Transient, t = 20 hr@ 29.6 kW, 127 Btulhr-ft 2Insolation, 104OF Ambient (load case # 6)

A Calculation No.: NUH32PHB-0402 Calculation Revision No.: 1AREVA Page: 41 of 65AN OCT 21 200918:28:22PLOr NO. 2NODA~L SOIIJTIOCI TIME=20SM =265.733SM =432.393265.733284.25mmm302.768 321.286339.804358.322_ 376.839-395.357413.875432.393(CCWP-FC--C with 32PHB, 29.6 kW -Off--Normal Transfer Transient RmnsAN OCT 21 200918:28:22PIDr NO. 1NODAL SOLUTIONTIhE=20S1N =265.733SMX =432.393265.733-284.25m 302.168321.286339.804m m 358.322m m 376.839395.357413.875432.393OUEP-FC--I with 32PB, 29.6 kW -Off-iormal Transfer Transient amFigure 6-4 DSC Shell Temperature Distribution

-Off-Normal Hot Transient, t -20 hr@ 29.6 kW, 127 Btulhr-ft 2Insolation, 1040F Ambient (load case #6)

Calculation No.: NUH32PHB0402 A Calculation Revision No.: 1AREVA Page: 42 of 65AN OCT 21 200918:44:53PI!r NO. 2NODL SOUMOic.P=6SUB =1Tfl'E=. 25SMN =282.039SW =433.465282.039298.864315.689332.514349.339EEZI366.165 EJ 382.99399. 815416.64433.465CflPP-FC-TC with 32FHB, 29.6 kW -15 Minute Fire Transient R=nsAN OCT 21 200918:44:53PLOT NO. 1NODL SOEL]rION STIEP=6SUB =1TIM--. 25I N =282.039SW =433.465282.039298.864315.689332.514I 349.339I__ 366.165I 382.99399.815*416.64433.465C2NPP-FC-TI with 32PMB, 29.6 kW -15 Minute Fire Transient RumsFigure 6-5 DSC Temperature Distribution

-Fire Accident, t = 15 min.@ 29.6 kW, 104°F Ambient (load case # 7)

A Calculation No.: NUH32PHB-0402 Calculation Revision No.: 1AREVA Page: 43 of 65AN OCr 21 200918:44:54PIXr NO. 4NODAL STEP=6SUB =1TIME=. 25TEPS =198.825=1372198.825329.133l 459.44EM 589.747= 120.055850.362U-]980.669 iiii12411372CaFF=-FC-TC with 29.6 kW -15 Minute Fire 7Tansient RAN T 21 200918:44:53PLOT NO. 3NODAL SOIwrIONSIEF=6SUB =1TIME=.25TEMPMN =198.825SM =1372198.825329.133459.44m 589.747720.055850.362_-- 980.669111112411372XCNPP-FC-WC with 32PHB, 29.6 kW -15 Minute Fire Transient RunsFigure 6-6 TC Temperature Distribution

-Fire Accident, t = 15 min.@ 29.6 kW, 104°F Ambient (load case # 7)

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 44 of 65AN CT 21 200918:53:33PIDr NO. 4NODAL SOLUTIONSTEP=-1SUB-=4TIME=1TEMWSMN =166.088SM =590.332166.088213.226260.364307.502m 354.64401.779448.917496.055543.193590.332CCNPP-FC-TC with 32PHB, 29.6 kW -Post Fire Steady StateAN OCr 21 200918:53:32P= NO. 3NODAL SOU3TIONSTEP=-1SUB--4TBhE=1TEMPSMN =166.088SMX =590.332m 166.088m213.226260.364307.502m 354.64401.779_-_ 448.917496.055543.193590.332CCNPP-FC-TC with 32PHB, 29.6 kW -Post Fire Steady StateFigure 6-7 TC Temperature Distribution

-Post-Fire

Accident, Steady State@ 29.6 kW, 127 Btu/hr-ft 2, 1040F Ambient (load case # 7)

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 45 of 65AN OCT 21 200918:53:32PLOr NO. 2NAL SOUTrIONS7EP--1SUB =4TIME=1S =437.138SM =692.066437.138465.463493.789522.114I. 550.439E2I 578.765I 607.09635.415663.741692.066MEFP-FC-TC with 32PHB, 29.6 kW -Post Fire Steady StateAN Wr 21 200918:53:31PLOT NO. 1NOAL SOLUTI OTRIE,=1S3N =437.138SMK =692.066437.138~465. 463493.789522.114550.439578.765607.09635.415692.066CCNEP'-FC-TC with 32PFB, 29.6 kW -Post Fire Steady StateFigure 6-8 DSC Shell Temperature Distribution

-Post-Fire

Accident, Steady State@ 29.6 kW, 127 Btulhr-ft 2, 1040F Ambient (load case # 7)

Calculation No.: NUH32PHB-0402 Revision No.: 1Page: 46 of 6514001200 4-0.u000800E0! Basket-U-DSC ShellInner LinerGamma Shield-)K-Structural Shell-*-Outer Shell400200-2818283848Time [hr)Figure 6-9Temperature History for Fire and Post-Fire Conditions

@ 29.6 kW, 1040F Ambient (load case # 7)

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 48 of 6

57.0 CONCLUSION

Based on the analyses presented in Section 5.0 and 6.0 the maximum duration for the on-site transfer operations of the CCNPP-FC TC with 32PHB DSC at 29.6 kW is 20 hours2.314815e-4 days <br />0.00556 hours <br />3.306878e-5 weeks <br />7.61e-6 months <br />.Further a time limit of 20 hours2.314815e-4 days <br />0.00556 hours <br />3.306878e-5 weeks <br />7.61e-6 months <br /> is also established as the maximum duration that the TC canbe left in the fuel building in a vertical orientation once the water in the DSCITC annulus isdrained.

If the transfer operations exceeds or are expected to exceed the above time limits,corrective actions such as forced air circulation or refilling of the TC/DSC annulus with'clean demineralized water should be initiated.

Table 7-1 summarizes the maximum temperatures of the TC components and the DSC shellfor vertical hot transient condition in the fuel building and for the off-normal hot horizontal transfer condition after 20 hours2.314815e-4 days <br />0.00556 hours <br />3.306878e-5 weeks <br />7.61e-6 months <br />.Table 7-1Maximum Temperatures of CCNPP-FC TC @ 29.6 kW,NO Forced Air Circulation Temperature

[OF]Vertical Hot Off-Normal HotComponent Load Case # 5 Load Case # 6 (2) Max. Allowable time = 20 hrMax. DSC Shell (1) 395 407 -Inner Shell 279 313 ---Gamma Shield 277 308 620 [8]Structural Shell 242 263Bulk Avg. Temp ofRadial Neutron Shield 201 214 280 [3]Bulk Avg. Temp ofTop Neutron Shield 232 186 280 [3]Bulk Avg. Temp ofBottom Neutron Shield 240 201 280 [3]Cask Lid 242 216 ---Cask Outer Shell 238 233 ---(1) The maximum DSC shell temperature is the temperature along the "DSC Shell" as shown in Figure5-3 and does not include the top and bottom end plates.(2) For the load cases shown in Table 4-1, Load cases # 1, 2, 3 and 4 are bounded by the Load Case #6 (off-normal hot horizontal transient transfer operations).

Table 7-2 summarizes the maximum temperatures for the TC components and the DSC shellwhen subjected to the fire accident conditions along with the time at which they occur.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 49 of 65Table 7-2Maximum Temperatures of CCNPP-FC TC for Accident Conditions Maximum Max. Allowable Components Time Tmeaue[~I

~ ITernperature

[°F] rOF]Max. DSC Shell c1 656Inner Shell 0_ 590 ---Gamma Shield __ 585 620 [8]Structural Shell to 568 ---Bulk Avg. Temp of.Radial Neutron Shield End of Fire 542 1300 [17]Bulk Avg. Temp ofT uto Shield End of Fire 640 1300 [17]Top Neutron ShieldBulk Avg. Temp ofBottom Neutron Shield End of Fire 441 1300 [17]Cask Lid End of Fire 910Cask Outer Shell End of Fire 1321 ---(1) The maximum DSC shell temperature is the temperature along the "DSC Shell" as shown in Figure 5-3 anddoes not include the top and bottom end plates.As seen the above tables, all design criteria specified in Section 4.5 are herein satisfied.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 50 of 658.0 LISTING OF COMPUTER FILESAll the runs in Revision 0 are performed using ANSYS version 10.0 [10] with operating system"Linux RedHat ES 5.1", and CPU "Opteron 275 DC 2.2 GHz" / "Xeon 5160 DC 3.0 GHz".Additional runs marked with revision bars in Table 8-2 are performed using ANSYS version10.0 [10] with operating system "RHEL5.6x64" on the AREVA HPC cluster with Intel X5675CPUs.A list of the files to create the finite element model of CCNPP-FC with 32PHB DSC is shownin Table 8-1.Table 8-1 List of Geometry Files Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 51 of 65A summary of ANSYS runs is shown in Table 8-2.Table 8-2Summary of ANSYS RunsDate I Time forRun Name Description Output FileInitial conditions of the CCNPP-FC TC with 32PHB 10/21/2009 DSC in vertical orientation.

6:16 PMOff-normal hot horizontal transient transfer of the 10/21/2009 32PHBTCOFN_TRANS CCNPP-FC TC with 32PHB DSC 6:28 PM32PHBTOVERTTRANS Vertical transient transfer of the CCNPP-FC TC 10/21/2009 with 32PHB DSC inside the Fuel Building 6:33 PM10/21/2009 32PHBTCOACCFIREINITIAL Initial conditions for the fire accident analysis 6:38 PM10/21/2009 32PHBTCOACCFIRE_15MIN 15 Minute Fire Accident Analysis 6:44 PM10/21/2009 32PHBTCOACCPF 24 Hour Post-Fire analysis 7:15 PM10/21/2009 32PHBTCOACCONS Post-Fire Steady State Analysis 6:53 PM32PHB TC OFN TRANS 20hr Map Temperature profile of 32PHB DSC for off-normal 10/21/2009 hot transient transfer conditions

@ 20 hours2.314815e-4 days <br />0.00556 hours <br />3.306878e-5 weeks <br />7.61e-6 months <br /> 6:44 PM32PHBTOVERTTRANS 20hr Map Temperature profile of 32PHB DSC for vertical 10/21/2009

---transient transfer conditions

@ 20 hours2.314815e-4 days <br />0.00556 hours <br />3.306878e-5 weeks <br />7.61e-6 months <br /> 6:49 PM32PHBTOACO NS Map Temperature profile of 32PHB DSC shell for post- 10/21/2009 fire steady state conditions 7:00 PM3Sensitivity analysis for effective density and 02/24/2010 32PHB TC OFNsTRANSpSENS specific heat changes 3:15 PMOff-normal hot horizontal transient transfer of the01/20/2015 32PHB_TCOFN1_TRANS CCNPP-FC TC with 32PHB DSC ( solar heat load 11:38 AMapplied on TC full circumference)

Temperature profile of 32PHB DSC shell for off-32PHB TC OFNITRANS_20hrMap normal hot transient transfer conditions

@ 20 01/20/2015 TO TM hours (solar heat load applied on TC full 2:51 PMcircumference)

Off-Normal Transfer Conditions

@ 20 hrs, 1040F 01/20/2015 32PHBOFN1

ambient, 29.6 kW (solar heat load applied on TC 3:30 PMfull circumference)

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 52 of 65ANSYS macros, and associated files used in this calculation are shown in Table 8-3.Table 8-3 Associated Files and MacrosFile Name Description Date I TimeHTOTHCL.MAC Total heat transfer coefficients for horizontal cylindrical surface 2/19/2009

-12:37 PMHTOTVPL.MAC Total heat transfer coefficients for vertical flat surface 2/19/2009 12:37 PMHTOTVCL.MAC Total heat transfer coefficients for vertical cylindrical surface 2/19/2009

-3:52 PMHTOTFIRE.MAC Total heat transfer coefficients for fire 9/12/2008 18:33 PM032PHBTCMat.inp Material properties for CCNPP-FC Cask 10/21/2009

-6:07 PMV32PHBTC Mat3.inp Material properties for CCNPP-FC Cask for post-fire steady 10/21/2009 2astate 6:12 PM32PHBTC PP.inp 9/16/2009 4:16 PM32PHB_TC_PP1.inp 1/20/2015 11:38 AM32PHBTCOPPVERT.inp Macros for Post-Processing Transient Runs 9/16/2009 5:48 PM32PHBTCPPFIRE.inp 9/16/2009 6:48 PM32PHBTCOPPPF.inp 9/22/2009 5:17 PMGamma Gap_32PHB-TC.xls Spreadsheet to Calculate gamma shield/structural shell gap 01/27/2010 10:17 AMGammaGap_32PHB-TC-2.xls Spreadsheet to Calculate gamma shield/structural shell gap for 01/27/2010 post-fire steady state conditions 10:17 AMCCNPP-FC TC-Material Prop.xls Spreadsheet for material properties used in the analysis 9/21/2009 1:41 PMFire History.xls Spreadsheet for Fire Temperature History Post Processing 10/27/2009 9:59 AMMacro for Creating Radiation Exchange between the DSC/TC 10/21/2009 32PHBTORAD_Horizontal.inp when the TC is in Horizontal Orientation 4:46 PM32PHB TC RADVertical.inp Macro for Creating Radiation Exchange between the DSC/TC 10/21/2009 when the TC is in Vertical Orientation 4:42 PM32PHB Model.db ANSYS Geometrical File for 32PHB DSC [21132PHB Matl.inp Material properties for 32PHB DSC with Helium [21]32PHB HLZC2.MAC Heat generation for 32PHB DSC, 29.6 kW [211Macro.mac Macro to get Maximum/Minimum temperatures

[21]Macro to list maximum and average 32PHB DSC component

[21]Results.mac tmeaue ______temperatures 32PHBTOOFN1_TRANS Mapped DSC shell temperature profile for off-normal hot 01/20/2015

_2OhrM T Fapcbdo transient transfer conditions

@ 20 hrs, solar heat load applied 2:51 PM_2_Map________cbdo

______ on TC full circumference 2:51_PM Calculation No.: NUH32PHB-0402 ACalculation Revision No.: 1AREVA Page: 53 of 65APPENDIX A TOTAL HEAT TRANSFER COEFFICIENTS Total heat transfer coefficient, ht, is used to combine the convection and radiation heattransfer together.

ht = hr + hcWhere,hr = radiation heat transfer coefficient (Btu/hr-in 2-OF)hc = free convection heat transfer coefficient (Btu/hr-in 2-°F)The radiation heat transfer coefficient, hr, is given by the equation:

hr = F " -Tmb [ e4 F1 .b 4) Btu/hr-in 2T-bFi[ Tu.. -TainhWhere,6 = surface emissivity F12 = view factor from surface 1 to ambient = 1a = 0.1714 x10-8 Btu/hr-ft 2-OR4T, = surface temperature (OR)Tamb = ambient temperature (OR)Surface emissivity values are discussed in Section 4.4.The following equations from Rohsenow handbook

[4] are used to calculate the freeconvection coefficients.

Horizontal Cylinders:

Ra =Gr Pr ; Gr =g 8 (T,,,- T.) DV 22fN ln(1u+2fNu T) withN-T- 1 0.13 -NuT =0.772 C, Ra114  ; f=1 (NuT)0.16 with C, = 0.515 for gases [4]Nut C, Ra 13Ct = 0.103 for air with Pr z, 0.71 [4]

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 54 of 65Nu = [(Nu,)- +(NU,)-I'mr with m=10 for 1010 <Ra <i10k = Nu k (Multiply by 0.1761/144 to convert from W/m2 -K to Btu/hr-in2

-F)Dwith2g = gravitational constant

=9.81 (m/s)P = expansion coefficient

= 1/T (1/K)T = absolute temperature (K)v = kinematic viscosity (m2/s)D = diameter of the horizontal cylinder (m)k = air conductivity (W/m-K)The above correlations are incorporated in ANSYS model via macro "HTOT_HCL.MAC" listed in Section 8.0.Vertical Flat Surfaces:

Ra=GrPr ; Gr =g/3(T. -T.) L?V2Nu, -2.0ln(1 + 2.0 /NuT) withNUT =5, Ra1 4 with C, =0.515 forgases

[4]Nu =Cv f Ra 13/(1+1.4x109 PriRa) withCv = 0.13Pr022 0.42 f =1(1+ 0.61 Pro`81)42 f =T0 .Nu=[(Nu,)-

+(Nut)m-Im with m=6 for 1<Ra<1012hc = Nuk (Multiply by 0.1761/144 to convert from W/m2 -K to Btu/hr-in2

-F)Lwithg = gravitational constant

=9.81 (m/s2)P = expansion coefficient

= 1/T (1/K)T = absolute temperature (K)v = kinematic viscosity (m2/s)L = height of the vertical surface (m)k = air conductivity (W/m-K)The above correlations are incorporated in ANSYS model via macro "HTOTVPL.MAC" listedin Section 8.0.

Calculation No.: NUH32PHB-0402 ACalculation Revision No.: 1AREVA Page: 55 of 65Vertical Cylindrical Surfaces:

Ra=GrPr ; Gr =g#(Tw -T.)LV 22.0lIn(1 + 2.01 NuT)Ra with C,=0.515 for gases [4]Nu with_ 1.8 LIDNupt = PlaRa UTNu, -In(1 + 4) NuNpate with Pl atN ui pateNut= Cv f Ra 13 /(1 + 1.4 x 109 Pr/Ra) withCv= (1+0.61Pr 0.22 f = 1.0 + 0.078kT-

--1Nu=[(Nu,)m

+(NU,)n'mIn/

with m=6 for 1<Ra<1012hc = Nu-k (Multiply by 0.1761/144 to convert from W/m2 -K to Btu/hr-in2

-F)Lwithg = gravitational constant

=9.81 (m/s )P3 = expansion coefficient

= V/T (1/K)T = absolute temperature (K)v = kinematic viscosity (m2/s)L = height of the vertical cylinder (m)D = Diameter of the Cylinder (m)k = air conductivity (W/m-K)The above correlations are incorporated in ANSYS model via macro "HTOTVCL.MAC" listed in Section 8.0.

A Calculation No.: NUH32PHB-0402 Calculation Revision No.: 1AREVA Page: 56 of 65APPENDIX B GAMMA SHIELD GAP JUSTIFICATION A 0.0452" radial air gap is assumed between the gamma shield (lead) and the TC structural shell within the finite element model described in Section 5.0. This air gap is due to thedifferential thermal expansion of the cask body and the gamma shield during the lead pour.The following assumptions are made for the verification of the gap:* The cask body has nominal dimension at 701F.* During the lead pour the TC body and lead are at 6200F.* The inner diameter of the gamma shell (lead) is equal to the outer diameter of the TCinner shell at thermal equilibrium.

The average coefficients of thermal expansion for SA-240 Type 304, SA516 GR70 and leadare listed in Table B-i.Table B-1Thermal Expansion Coefficients Temperature SA240 Type 304 SA516 GR70(OF) a a(in/in-°F)

[11] (in/in-°F)

[11]70 8.46E-06 5.42E-06200 8.79E-06 5.89E-06300 9.OOE-06 6.26E-06400 9.19E-06 6.61E-06500 9.37E-06 6.91E-06600 9.53E-06 7.17E-06700 9.69E-06 7.41 E-06Temperature Lead(OF) a(in/in-°F)

[11]70 16.07 E-6100 16.21 E-6175 16.58 E-6250 16.95 E-6325 17.54 E-6440 18.50 E-6620 20.39 E-6The density of lead as a function of temperature is listed in Table.Table B-2Density of LeadTemperature Density ;1 1] Temperature Density(K) (OF) (Ibm/in100 11,520 -280 0.4162150 11,470 -190 0.4144200 11,430 -100 0.4129250 11,380 -10 0.4111300 11,330 80 0.4093400 11,230 260 0.4057500 11,130 440 0.4021600 11,010 620 0.3978 Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 57 of 65The volume within the "lead cavity" is found by determining the cask body dimensions at6200F. As no gaps will be present between the molten lead and the cask body, this volume isalso equal to the volume of lead at 6200F. The mass of the lead that fills the lead cavity at620°F is then determined.

The dimensions of the "lead cavity" are calculated based on cask body temperature.

Atemperature of 305°F is considered for the cask body. This temperature is lower than themaximum cask inner shell temperature shown in Table 6-1. Since the gap size increases atlower temperatures, the above chosen value is conservative.

From the mass of the lead andits density at 3050F, the lead volume is determined.

The length of the gamma shield at the TC body temperature is calculated based on thermalexpansion coefficients listed in Table B-1. The lead volume is used to determine themaximum size of the air gap adjacent to the lead. See Spreadsheet "GammaGap_32PHB-TC.xls" listed in Table 8-3 for the air gap calculations shown below.Determination of Lead MassXSS304, 620 =9.56 x 106o in/in-°F at 620°F (via linear interpolation, Table B-1)otCS516, 620 = 7.22 x 10-6 in/in-°F at 620°F (via linear interpolation, Table B-i)Plead, 620 = 0.3978 Ibm/in3 at 620°F (Table B-2)Rin = inner radius of lead cavity at 700F= 34.75"Rout = outer radius of lead cavity at 70°F = 38.75"Lcav4ty = length of lead cavity at 70°F = 165.50"Rin, 620 = (Rin)(1 +(X ss304, 620)(AT)) = 34.9328"Rout, 620 = (Rout)(1

+(C CS516, 62o)(AT)) = 38.9038"Lcavity, 620 = (Lcavity)(1

+(C CS516, 620)(AT)) = 166.1570" Vcavity = Vlead, 620 = (7c)(Rout,62o2

-Rin,6202)(Lcavity, 620) = 153,055.5 in3Mlead = (Vlead, 620)(Plead, 620) = 60,878.5 IbmDetermination of Lead GapXss3o4, 305 = 9.01 x 10-6 in/in-°F at 305°F (via linear interpolation, Table B-1)XcS516, 305 = 6.28 x 10-6 in/in-°F at 305°F (via linear interpolation, Table B-I)OXlead, 620 = 20.39 x 10-6 in/in-°F at 620°F (via linear interpolation, Table B-1)OXClead, 305 = 17.38 x 10-6 in/in-°F at 305°F (via linear interpolation, Table B-i)Plead,305

= 0.4048 Ibm/in3 at 305°F (via linear interpolation from Table B-2)Rin,SS304, 305 = (Rin)(l+(ass304, 305)(AT)) = 34.8236"Rout, cS516, 305 = (Rout)(1

+(a CS516, 3o5)(AT)) = 38.8072" 4A Calculation No.: NUH32PHB-0402 Calculation Revision No.: 1AREVA Page: 58 of 65Llead, 305 = (Lcavity, 620)/[1 +(c, lead,620)(

620 -70)]*(1 +(a lead,305)(

305 -70))= 164.9855" Vlead, 305 = Mlead / Plead, 305 = 150,391.8 in3Since Rin,SS304, 305 = Rin, lead, 305, then :Vlead,305

= (7)(Rout, lead,305

" Rin, SS304, 305 )(Llead, 305)It gives:Rout, lead, 305 = 38.7664"Air gap = Rout, CS516, 305 -Rout, lead, 305 = 38.8072 -38.7664 = 0.0408"The assumed air gap of 0.0452" is larger than the above calculated gap. Therefore, using agap of 0.0452" is conservative to maximize the 32PHB DSC shell temperature.

Based on the above methodology, the air gap is recomputed for the post-fire steady stateanalysis based on a temperature of 590°F for the cask body. This temperature is themaximum cask inner shell temperature shown in Table 6-2. The computed air gap betweenthe lead and the structural shell is 0.004". To account for the effect in the reduction of thecomputed air gap between the gamma shield and structural shell from 0.0412" to 0.004", theeffective conductivity of air in the region is increased by a factor of 4. This factor of 4corresponds to an air gap of 0.011" (0.0452/4

= 0.0113")

and is therefore conservative for thepost-fire steady state conditions.

Calculation No.: NUH32PHB-0402 Calculation Revision No.: 1AREVA Page: 59 of 65APPENDIX C DSC SHELL TEMPERATURE During the handling and vacuum drying operations, the DSC outer shell is in contact withwater in annulus between the DSC and the transfer cask. The annulus is open toatmospheric pressure.

To bound the problem, it can be assumed conservatively that the total heat load from theassemblies flows to water in the annulus and no heat dissipation to ambient occurs. As longas the DSC shell is in contact with water, the decay heat will be used to evaporate andeventually boil the water in annulus.

The water bulk temperature remains constant at 212°F(1 00°C) if water starts to boil.The following calculation shows that the maximum allowable heat load for 32PHB DSC (29.6kW [11]) is not adequate to boil the water in annulus.

Therefore, the maximum bulktemperature for water in annulus is bounded by boiling temperature of 212°F (1000C).Observations show that the hot surface temperature in contact with boiling water is typically 10-150C higher than the boiling temperature for heterogeneous nucleation process [4, page15.9]. The temperature gradient between the hot surface and the boiling water is defined asATsat.ATsat. = (Tw -Tsat) > 10 to 150C (C.1)T, = hot surface temperature (0c)Tsat = saturated water temperature

= 1000C at atmospheric pressureUnder boiling water conditions, ATsat can be calculated using the following correlation from [4,page 15.46].-" ~0.33 .AT,., Cs_ il1i,3lg ,[-1g (C.2)CSF = liquid/surface constant

= 0.013 [4] 2qDSC" = heat flux from hot surface of one fuel rod = 1320 W/m (see below)p = dynamic viscosity of saturated water = 2.79E-4 N.s/m2 [4]ilg = latent heat of vaporization

= 970.3 Btu/lbm [4] = 2.257E6 J/kgc = surface tension of water = 0.059 N/M [4]g = gravity constant

= 9.8 m/s2 [4]p= density of saturated water = 958 kg/mi3 (vI = 1.0435E-3 m3/kg [19])Pg = density of saturated steam= 0.598 kg/mi3 (Vg = 1.673 m3/kg [19])k= conductivity of saturated water = 0.68 W/m-K [4]All the properties are at 1000C.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 60 of 65The heat flux from DSC outer shell (qDsc") is calculated as follows.qDSC" -OQ -1320W/m2 (C.3);r OD0sc L.ann1Q = maximum heat load per DSC = 29.6 kW [11]ODosc = Outer DSC shell diameter

= 67.25" [11] = 1.708 mLann = water height in annulus = DSC height -12" = 176.50 [14, Drawing NUH32PHB-30-1]-12"

= 164.5" = 4.178 mIt is assumed that approximately 12" of water is drained from the DSC top before the weldingoperation is started [3, Section 5.1.1.3].

Using qDSC" in equation (C.2) gives the ATsat for annulus.ATsatan.

= 2.1°C (C.4)ATsat,ann is much lower than the required temperature gradient of 10 to 150C to boil the water.It concludes that no boiling will occur within the annulus between the DSC shell and transfercask.

A Calculation No.: NUH32PHB-0402 Calculation Revision No.: 1AREVA Page: 61 of 65APPENDIX D SENSITIVITY OF THE EFFECTIVE DENSITY AND SPECIFIC HEAT OF THEHOMOGENIZED BASKETThis section presents a sensitivity analysis of the maximum temperatures in the CCNPP-FCTC to the changes in the effective density and specific heat of the homogenized basketconsidered in the transient analysis.

During the design process of the 32PHB DSC system, the weight of the fuel assembly isdecreased which affects the effective specific heat and density of the homogenized basketconsidered in this calculation and shown in Table 4-10. The updated effective specific heatand density of the homogenized basket used in this appendix from [13] are listed in TableD-1.Table D-1 Effective Density and Specific Heat [13]Temp Cp eff eff(OF) (Btu/Ibm-°F)

(lb/in*)70 0.097100 0.097200 0.099300 0.101400 0.102 0.126500 0.102600 0.103700 0.103800 0.103900 0.1031000 0.104Table D-2 presents a comparison on the maximum temperatures using the effective specificheat and density of the homogenized basket listed in Table 4-10 to those listed in Table D-1.As seen from Table D-2, the maximum difference in the DSC shell temperature is 1OF and isnegligible.

Therefore, the CCNPP-FC TC analysis and the resulting DSC temperature profilesused in the 32PHB DSC/Basket analysis in [13] for the fuel cladding temperatures remainbounding.

Calculation No.:NUH32PHB-0402 Revision No.:1Page: 62 of 65Table D-2Sensitivity of Maximum Temperatures toEffective Density and Specific HeatTemperature

[OF]Component Off-Normal Hot (Load Case # 6) Difference (Original Model,(Sensitivity Run) Table 6-1) Tsensitivity

-Toriginal time = 20 hrMax. DSC Shell 408 407 +1Inner Shell 314 313 +1Gamma Shield 308 308 0Structural Shell 264 263 +1Bulk Avg. Temp ofRadial Neutron ShieldBulk Avg. Temp ofTop Neutron ShieldBulk Avg. Temp ofBottom Neutron ShieldCask Lid 217 216 +1Cask Outer Shell 233 233 0 Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 63 of 65APPENDIX E SENSITIVITY STUDY OF APPLYING SOLAR HEAT LOAD TO FULLCIRCUMFERENCE OF THE CASK IN THE HORIZONTAL ORIENTATION The thermal evaluation methodology presented in Section 5.1 considers that the lower halvesof the CCNPP-FC TC cylindrical surfaces are not exposed to insolance during outdoortransfer operations in horizontal orientation.

This evaluation considers a conservative solarheat load of 127 Btu/hr-ft2 for a 24 hour2.777778e-4 days <br />0.00667 hours <br />3.968254e-5 weeks <br />9.132e-6 months <br /> period as shown in Table 5-2. In comparison, 10 CFR 71.71 [11 specifies a maximum solar heat load of 400 gcal/cm for curved surfacesand 200 gcal/cm for vertical flat surfaces over a 12 hour1.388889e-4 days <br />0.00333 hours <br />1.984127e-5 weeks <br />4.566e-6 months <br /> period.However, because of the large thermal inertia of the TC, the insolation values listed in10 CFR Part 71.71 [1] can be averaged over a 24-hour day assuming steady-state conditions as noted in Section 4.5.3 of NUREG 1536 [22]. Table E-1 presents a comparison of the solarheat load values from 10 CFR 71.71 [1] to those used in the thermal evaluation of CCNPP-FC TC. As seen from the table, the solar heat load used for CCNPP-FC TC is approximately twice of the solar heat load from 10 CFR 71.71 [1] for curved surfaces and four times forvertical flat surfaces.

Due to this large conservatism, the use of the solar heat load only onthe top half of the TC should be acceptable.

Table E-1 Comparison of Solar Heat Load between 10 CFR 71.71 vs Design BasisValues for CCNPP-FC TC10 CFR 71.71 [1] Insolation used for CCNPP-FC TC(See Table 5-2)Total Insolation Solar Heat Flux Solar Heat Flux(gcal/cm2) (1) (Btu/hr_ft

2) (2) (Btu/hrft

2) (2)Curved Surface 400 61.4 127Vertical Flat Surface 200 30.7 127Note (1): Values from 10 CFR 71.71 (c) of [1].Note (2): Average values over a 24-hour period.However, to remove any uncertainty about applying the solar boundary conditions only on theupper half of the TC surfaces for the outdoor transfer operations in the horizontal orientation, a sensitivity analysis is performed by applying the solar heat load on all exterior surface areasof the TC using the insolation values from 10 CFR 71.71 [1]. The insolation values from 10CFR 71.71 are averaged over 24 hours2.777778e-4 days <br />0.00667 hours <br />3.968254e-5 weeks <br />9.132e-6 months <br /> and multiplied by the surface absorptivity factor tocalculate the solar heat flux. The total solar heat flux values applied in the sensitivity analysisare listed in Table E-2.

9-.Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 64 of 65Table E-2 Solar Heat Flux Applied in the Sensitivity AnalysisForm and Location of Total Insolation Solar Heat Flux Solar Total Solar Heat FluxSurface (gcal/cm2)

(1) (Btu/hr-ft

2) (3) Absorptivity (2) (Btu/hr-in 2)Curved Surface 400 61.4 0.587 0.250Vertical Flat Surface 200 30.7 0.587 0.125Note (1): Values from 10 CFR 71.71 (c) of [1].Note (2): Value from Table 5-2.Note (3): Average values over a 24-hour period.A review of the various load cases from transfer operation in Table 4-1 shows that LoadCase # 6 bounds other outdoor transfer operations with insolation.

Therefore, Load Case # 6(Table 4-1, off-normal horizontal hot transfer conditions) is re-evaluated in this sensitivity analysis by applying the solar heat load shown in Table E-2 on all exterior surfaces of the TC.The same methodologies described in Section 5.1 of this calculation and Section 5.0 of [13]for thermal evaluation of the CCNPP-FC TC and 32PHB DSC, respectively, are used in thesensitivity analysis to predict the maximum temperatures for the TC and DSC components including fuel cladding.

Table E-3 presents a comparison of the maximum temperatures of the fuel cladding, DSCcomponents and TC components with solar heat load applied to the full circumference of theTC to the design basis values listed in Table 7-1 of this calculation and Table 6-1/Table 6-2of [13].As seen from Table E-3 for the various TC components, the maximum temperatures retrieved from the sensitivity analysis (solar insolation from 10 CFR 71.71 [1] applied over thefull circumference) vary slightly compared to the design basis temperatures determined witha solar heat load 127 Btu/hr-ft (applied over the upper half of the curved surfaces and on allvertical surfaces).

However, all temperatures remain below their allowable limits and there isno adverse impact due to the application of solar heat load over the entire circumference ofthe TC outer surfaces.

Further, as described in Section 5.1.2 of [21], thermal stress evaluation of the TC loaded with32PHB DSC is based on design basis thermal stress evaluation of the TC loaded with 32PDSC, which is documented in [20]. As discussed in Section 3.4.1 of Appendix 1 in [20], thethermal stress analysis is based on a design temperature for the TC of 400 OF, which ishigher than all the temperatures for the TC components reported in Table E-3. Therefore, there is no impact of small temperature increases observed for some of the TC components on the structural analysis.

In addition, as seen from Table E-3, there is no impact on the maximum temperature of thefuel cladding due to the change in the solar heat load boundary conditions.

Further, themaximum temperatures for the various DSC components are either reduced or not impacteddue to the change in the solar heat load boundary conditions.

This shows that the fuel

-qCalculation No.: NUH32PHB-0402 A Calculation Revision No.: 1AREVA Page: 65 of 65cladding and DSC components are not impacted due to the change in the application of thesolar heat load.Therefore, the application of the conservative solar heat load of 127 Btu/hr-ft2 only to the tophalf of the transfer cask during outdoor transfer operation is adequate to evaluate the thermalperformance of the 32PHB DSC in CCNPP-FC TC.Table E-3 Sensitivity of Maximum Temperatures of Fuel Cladding, Components to Solar Heat Load Boundary Conditions TC and DSCTemperature

[0F]Off-Normal Hot (W 20 hr (Load Case # 6)Sensitivity RunDesign Basis Run(See Table 7-1)TC Surface Exposed to Solar Full Circumference Top Half Difference Heat LoadTC Component Tsensitivity

-TDesign BasisInner Shell 318 313 +5Gamma Shield 312 308 +4Structural Shell 270 263 +7Bulk Avg. Temp ofRadial Neutron ShieldBulk Avg. Temp ofTop Neutron ShieldBulk Avg. Temp of 186 201 -15Bottom Neutron ShieldCask Lid 217 216 +1Cask Outer Shell 236 233 +3DSC Component Table 6-1/Table 6-2 TSensitivity

-of [13] TDesign BasisFuel Cladding 728 728 0Basket Plates 709 709 0Al/Poison Plate 708 708 0Basket Rail 470 472 -2Top Shield Plug 343 346 -3Bottom Shield Plug 354 358 -4Cavity Gas (Average) 515 516 -1Fuel Cladding (Average) 566 566 0Max. DSC Shell 405 408 -3