ML12006A136

Enclosure 7 - Tn Calculation NUH32PHB-0402, Thermal Evaluation of Nuhoms 32PHB Transfer Cask for Normal, Off-Normal, and Accident Conditions

ML12006A136
Person / Time
Site:	Calvert Cliffs
Issue date:	04/09/2011
From:	Venigalla V AREVA, Constellation Energy Nuclear Group, Transnuclear, Calvert Cliffs
To:	Office of Nuclear Material Safety and Safeguards
References
NUHOMS 32PHB, Rev. 0
Download: ML12006A136 (63)

Text

ENCLOSURE7 TN Calculation NUH32PHB-0402, Thermal Evaluation of NUHOMS 32PHB Transfer Cask for Normal, Off-Normal, and Accident Conditions Calvert Cliffs Nuclear Power Plant, LLC December 8, 2011

A Form 3.2-1 Calculation No.: NUH32PHB-0402 A REVA Calculation Cover Sheet Revision No.: 0 TRANSNUCLEAR INC, TIP 3.2 (Revision 4) Page: 1 of 62 DCR NO (if applicable) : N/A PROJECT NAME: NIJI-10IOS'32if)HI3 System PROJECT NO: 10955 CLIENT: Ctp uNres- Calvert CliffNuclear Power Plant (CCNPP)

CALCULATION TITLE:

Thermal Evaluation of NUHOMS 32PHB Transfer Cask for Normal, Off Normal, and Accident Conditions

SUMMARY

DESCRIPTION:

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

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

Yes n] No [g (explain below) Licensing Review No.:

This calculation is prepared to support a Site Specific License Application by CCNPP that will be reviewed and approved by the NRC. Therefore, a 10CFR72.48 licensing review per TIP 3.5 is not applicable.

Software Utilized (subject to test requirements of TIP 3.3): Version:

ANSYS 10.0 Calculation is complete:

Originator Name and Signature: Venkata Venigalla Date: 0 Calculation has been checked for consistency, completeness and correctness:

Checker Name and Signature: Davy Qi )4 /O9&/iZP(

0SDate:

Calculation is approved for use:

Project Engineer Name and Signature: Kamran Tavassoli ( Date: /1

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 2 of 62 REVISION

SUMMARY

AFFECTED AFFECTED REV. DESCRIPTION PAGES Computational 1/0 0 Initial Issue All All

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 3 of 62 TABLE OF CONTENTS Paqe 1 .0 P urp o s e ............................................................................................................................. 6 2.0 References ........................................................................................................................ 7 3.0 Assum ptions and Conservatism .................................................................................... 9 3.1 CCNPP-FC TC Model ........................................................................................... 9 3.2 32PHB DSC Model ............................................................................................. 10 4.0 Design Input .................................................................................................................... 11 4.1 Design Load Cases ......................................................................................  :......... 11 4.2 Major Dim ensions in the CCNPP-FC TC Model ................................................. 11 4.3 Therm al Properties of Materials ......................................................................... 12 4.4 Surface Properties of Materials ........................................................................... 19 4.5 Design Criteria .................................................................................................... 19 5.0 Methodology .................................................................................................................... 21 5.1 CCNPP-FC TC Model ......................................................................................... 21 5.2 Fire Accident ...................................................................................................... 23 5.3 Effective Conductivity of Slide Rails .................................................................. 31 5.4 Effective Therm al Properties of DSC End Plates ............................................... 31 5.4.1 Top Shield Plug Assembly and Top Cover Plate 31 5.4.2 Bottom Shield Plug Assembly 33 6.0 Results and Discussion ............................................................................................. 35 7.0 Conclusion ...................................................................................................................... 48 8.0 Listing of Com puter Files ........................................................................................... 50 APPENDIX A Total Heat Transfer Coefficients ................................................................ 53 APPENDIX B Gam m a shield gap justification .................................................................... 56 APPENDIX C DSC Shell Tem perature ................................................................................ 59 APPENDIX D Sensitivity of the Effective Density and Specific Heat of the Homogenized Basket

........................................................................................................................................ 61

A Calculation No.: NUH32PHB-0402 AREVA Calculation RevisionNo.: 0 TRANSNUCLEAR INC. Page: 4 of 62 LIST OF TABLES Page Table 4-1 Design Load Cases for 32PHB DSC in CCNPP-FC TC without FC ............... 11 Table 4-2 Major Dimension of 32PHB DSC in CCNPP-FC TC model [14] ................... 12 Table 4-3 List of Materials in the CCNPP-FC TC Model ............................................... 13 Table 4-4 Stainless Steel, SA 240, Type 304 / SA 182 Type F304N [6-8] ..................... 14 Table 4-5 Carbon Steel, SA 516, Gr.70 [7, 9] ............................................................... 14 Table 4-6 Gamma Shield, ASTM B29 Lead [5] ............................. 14 Table 4-7 Castable Neutron Shield, NS-3 [12, 15] ......................................................... 15 Table 4-8 A ir Therm al Properties [4] ............................................................................. 16 Table 4-9 Helium Thermal Conductivity [4] .................................................................... 17 Table 4-10 Thermal Properties of Homogenized Basket() 1 [13] ....................................... 17 Table 4-11 Effective Conductivity of Top Shield Plug and Top Cover Plate .................... 18 Table 4-12 Effective Conductivity of Bottom Shield Plug ................................................. 18 Table 4-13 Effective Conductivity of Slide Rail ............................................................... 19 T able 5-1 Decay Heat Load ......................................................................................... .. 21 T able 5-2 S olar Heat Flux ........................................................................................... .. 22 Table 5-3 Distance between 32PHB DSC and TC Centerline ....................................... 22 Table 5-4 Thickness and Weights of the Top End Assembly ......................................... 31 Table 5-5 Thickness and Weights of the Bottom End Assembly .................................... 34 Table 6-1 Maximum Temperatures of CCNPP-FC TC @ 29.6 kW, NO Forced Air C irc u la tio n .................................................................................................. . . 36 Table 6-2 Maximum Temperatures of CCNPP-FC TC for Accident Conditions ............ 37 Table 7-1 Maximum Temperatures of CCNPP-FC TC @ 29.6 kW, NO Forced Air C ircu la tio n .................................................................................................. . . 48 Table 7-2 Maximum Temperatures of CCNPP-FC TC for Accident Conditions ............ 49 Table 8-1 List of Geom etry Files .................................................................................. 50 Table 8-2 Summary of ANSYS Runs ........................................................................... 51 Table 8-3 Associated Files and Macros ............  :....................... 52 Table B-1 Thermal Expansion Coefficients .................................................................... 56 T able B-2 Density of Lead ........................................................................................... .. 56 Table D-1 Effective Density and Specific Heat [13] ...................................................... 61 Table D-2 Sensitivity of Maximum Temperatures to Effective Density and Specific He a t ................................................................................................................... 62 LIST OF FIGURES Page Figure 5-1 Location of 32PHB DSC within CCNPP-FC TC ............................................ 24 Figure 5-2 Finite Element Model of CCNPP-FC TC with 32PHB DSC ........................... 25 Figure 5-3 CCNPP-FC TC Finite Element Model, Components ...................................... 26 Figure 5-4 Gaps in CCNPP-FC TC Model .................................................................... 27 Figure 5-5 CCNPP-FC TC Finite Element Model, Cross Section ................................... 28 Figure 5-6 Typical Decay Heat and Insolance Boundary Conditions ............................. 29 Figure 5-7 Typical Convection and Radiation Boundary Conditions .............................. 30

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 5 of 62 Figure 6-1 TC Temperature Distribution - Vertical Loading Transient, t = 20 hr @

29.6 kW, No Insolation, 100°F Ambient (load case # 5) ............................... 38 Figure 6-2 DSC Shell Temperature Distribution - Vertical Loading Transient, t = 20 hr

@ 29.6 kW, No Insolation, 100°F Ambient (load case # 5) .......................... 39 Figure 6-3 TC Temperature Distribution - Off-Normal Hot Transient, t = 20 hr @ 29.6 kW, 127 Btu/hr-ft 2 Insolation, 1040 F Ambient (load case # 6) ....................... 40 Figure 6-4 DSC Shell Temperature Distribution - Off-Normal Hot Transient, t = 20 hr

@ 29.6 kW, 127 Btu/hr-ft 2 Insolation, 104 0 F Ambient (load case # 6) ....... 41 Figure 6-5 DSC Temperature Distribution - Fire Accident, t = 15 min. @ 29.6 kW, 104'F Am bient (load case # 7) ..................................................................... 42 Figure 6-6 TC Temperature Distribution - Fire Accident, t = 15 min. @ 29.6 kW, 104 0F A m bient (load case # 7) ...................................................................... 43 Figure 6-7 TC Temperature Distribution - Post-Fire Accident, Steady State @ 29.6 kW , 127 Btu/hr-ft2 , 1040 F Ambient (load case # 7) ....................................... 44 Figure 6-8 DSC Shell Temperature Distribution - Post-Fire Accident, Steady State

@ 29.6 kW, 127 Btu/hr-ft 2 , 104 0F Ambient (load case # 7) ........................... 45 Figure 6-9 Temperature History for Fire and Post-Fire Conditions @ 29.6 MW, 104'F A m bient (load case # 7) ............................................................................... 46 Figure 6-10 Bulk Average Temperature History of NS-3 in TC for Fire and Post-Fire Conditions @ 29.6 kW, 104 0 F Ambient (load case # 7) ................................ 47

A Calculation No.: NUH32PHB-0402 AREVA Calculation RevisionNo.: 0 TRANSNUCLEAR INC. Page: 6 of 62 1.0 PURPOSE This calculation determines the maximum component temperatures of the Calvert Cliff Nuclear Power Plant Onsite Transfer Cask (CCNPP-FC TC) loaded with 32PHB DSC at 29.6 kW without forced convection. It also establishes the maximum time limits for transfer operations of a 32PHB DSC with 29.6 kW heat load in CCNPP-FC TC before initiation 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 for 32PHB DSC/Basket model to be evaluated in Reference [13].

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 7 of 62

2.0 REFERENCES

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

2 U.S. Code of Federal Regulations, Part 72, Title 10, "Licensing Requirements for the Independent Storage of Spent Nuclear Fuel and High-Level Radioactive Waste".

3 Calvert Cliffs Independent Spent Fuel Storage Installation UPDATED SAFETY ANALYSIS REPORT, Rev.17.

4 Rohsenow, Hartnett, Cho, "Handbook of Heat Transfer", 3 rd Edition, 1998.

5 Rohsenow, Hartnett, Ganic, "Handbook of Heat Transfer Fundamentals", 2 rd 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, 5 th Edition, 1973.

9 American Institute of Steel Construction, "AISC Manual of Steel Construction," 9 th Edition.

10 ANSYS computer code and On-Line User's Manuals, Version 10.0.

11 Design Criteria Document, "Design Criteria Document (DCD) for the NUHOMS6 32PHB System for Storage", Transnuclear, Inc., NUH32PHB.0101 Rev. 0.

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 and Transfer Conditions", Transnuclear, Inc., NUH32PHB-0403, Rev. 0.

14 Calculation, "NUHOMS 32PHB Weight Calculation of DSC/TC System",

Transnuclear, Inc., NUH32PHB-0201, Rev. 0 15 M. Greiner, S. Shin, B. Snyder and R.A. Wirtz, 1995, "Transportation Package Thermal and Shielding Response to a Regulatory Fire", Proc. 6th International High Level Radioactive Waste Management Conference, April 30-May 5, Las Vegas, NV, pp. 538-541.

16 Siegel, Howell, "Thermal Radiation Heat Transfer", 4th Edition, 2002.

A Calculation No.: NUH32PHB-0402 AREVA Calculation RevisionNo.: 0 TRANSNUCLEAR INC. Page: 8 of 62 17 GESC, NAC International, Atlanta Corporate Headquarters, 655 Engineering Drive, Norcross, Georgia (Engineering Report # NS3-020, Effects of 1300OF on Unfilled NS-3, while Bisco Products, Inc., 11/84).

18 Gregory, et al., "Thermal Measurements in a Series of Long Pool Fires", SANDIA Report, 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.

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 9 of 62 3.0 ASSUMPTIONS AND CONSERVATISM The following assumptions and conservatism are considered in the calculation.

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

The decay heat load is simulated by heat generation distributed uniformly over the basket length 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 the 32PHB DSC. This assumption reduces the axial heat transfer and maximizes the DSC shell temperature, which in turn results in higher fuel cladding temperature.

For the transfer operations in horizontal orientation, the lower halves of the CCNPP-FC TC cylindrical surfaces are not exposed to insolance. No solar heat flux is considered over these surfaces. To remove any uncertainty about the solar impact on the vertical surfaces, the entire 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 centered within the transfer cask and heat transfer through the slide rails is neglected. Further the top and bottom TC are modeled as adiabatic surfaces with only the outer shell surface dissipating 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 by using 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 flange c) 0.025" radial gap between the top cover plate and the top flange d) 0.75" radial gap between the bottom cover plate and the bottom end plate e) 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 neutron shield (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 in APPENDIX B.

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 10 of 62 Gaps "b" and "c" between the top cover plate and the top flange account for the thermal resistance between bolted components.

The radial gap "d" of 0.75" between the bottom cover plate and bottom end plate is larger than the nominal gap. This is conservative since the hot gaps at thermal equilibrium would be smaller.

The axial gaps "e" of 0.0625" between the DSC end plates maximizes the radial heat transfer through 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 adjacent materials to allow heat input into the cask from the fire. The gaps are restored for the post-fire conditions.

3.2 32PHB DSC Model The assumptions and conservatism considered for 32PHB DSC model are the same as those described in [13], Section 3.0, except those noted below.

During loading operations, the water level in cask/DSC annulus is maintained 12" below the DSC top and is open to atmospheric pressure until the DSC is sealed. The water in the annulus 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 that the 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 the initial conditions in the CCNPP-FC TC when the TC is in the vertical orientation and the DSC/TC annulus is filled with water. See APPENDIX C for justification of DSC shell temperature.

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 11 of 62 4.0 DESIGN INPUT 4.1 Design Load Cases The following design cases in Table 4-1 are analyzed in this calculation to determine the thermal performance of CCNPP-FC TC with 32PHB DSC at 29.6 kW and without forced convection (FC). The load cases are based on requirements in [11].

Table 4-1 Design Load Cases for 32PHB DSC in CCNPP-FC TC without FC Case Operation Condition Description Note s Ambient Temperature Insolation Airflow

[OF] [Btu/hr-ft 2] [cfm]

1 Normal Normal Hot (3) 104 82 0 2 Normal Normal Cold (3) -8 0 0 3 Off-Normal Off-Normal Hot (3) 104 127 0 4 Off-Normal Off-Normal Cold t3 -8 0 0 5 Normal Vertical Operations, Transient (1) 100 0 0 6 Off-Normal Off-Normal Hot, Transient (1) 104 127 0 7 Accident Fire Accident (2) 104/1475/104 127 0 Notes:

1) Initial steady-state conditions with 212OF water assumed in the DSC/TC annulus. At time t=0, the water is drained, no forced air circulation is available, and the system begins to heat up.

2) 15 Minute Fire Transient. 10CFR71. 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 transfer operations without forced air circulation). Post-fire condition assumes the decomposition of the neutron shield 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 Model Major dimension of 32PHB DSC used in the CCNPP-FC TC model are listed in Table 4-2 below.

All other dimensions are based on nominal dimensions of CCNPP-FC transfer cask drawings listed in DWG NUH32PHB-30-1 1.

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 12 of 62 Table 4-2 Major Dimension of 32PHB DSC in CCNPP-FC TC model [14]

DSC Component Length

[in]

Bottom End Plates Bottom Lead Casing Plate 0.50 Bottom Lead Shielding 4.25 Bottom Cover Plate 1.75 Top End Plates Lead Plug Top Casing Plate 0.75 Top Lead Shielding 4.00 Top Inner Cover Plate 1.50 Outer Top Cover Plate 1.25 Cavity Length 158.75(')

DSC Length 172.75 (w/o grapple)

Basket height 158.00 Note 1: 158.63"is the minimum length for DSC the cavity as shown in [14]. However, the nominal length of 158.75" used in this calculation [Nominal Cavity Length = DSC Length (172.75") - Total thickness 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 in CCNPP-FC TC model are listed in Table 4-4 through Table 4-13 for reference.

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 13 of 62 Table 4-3 List of Materials in the CCNPP-FC TC Model Component Mat # in ANSYS Model Material Transfer Cask Properties Bottom Cover Plate (10"thick) 101 SA240 Type 304 Bottom End Plate (0.75" thick) 102 SA240 Type 304 Bottom Support Ring 103 SA182 F304N Bottom Cover NS-3 (3.5" thick) 104 NS-3 Plate for Bottom Cover (0.5" thick) 105 SA240 Type 304 Bottom Castable NS-3 (3.63" thick) 106 NS-3 Bottom Cover Plate (2" Thick) 107 SA240 Type 304 Ram Access Machined Ring 108 SAl 82 Type F304N Plate for Top Cover (0.25" thick) 109 SA240 Type 304 Top Cover NS-3 (3" thick) 110 NS-3 Top Cover Plate (3" thick) 111 SA240 Type 304 Inner Shell (0.75" thick) 112 SA240 Type 304 Lead Shielding (Gamma Shield, 4" 113 ASTM B29 thick)

Structural Shell (1.5" & 2" thick) 114 SA516 GR70 Top Flange 115 SA182 Type F304N Neutron Shield Panel (0.25" thick) 116 SA240 Type 304 NSP Support Angle (0.25" thick) 117 SA240 Type 304 Radial Neutron Shield (4" thick) 118 NS-3 Rails (0.12" thick) 119 Nitronic SeScin53 60 (Effective Properties used.

See Section 5.3)

DSC Properties DSC Shell 301 SA240 Type 304 DSC Bottom Shield Plug Assembly 302542 Effective Properties used, See Section 5.4.2 DSC Top Shield Plug Assembly 303 Effective Properties used, See Section

+ Top Outer Cover Plate 5.4.1 DSC Helium Gap 304 Helium DSC Basket 305 Homogenized Region, Effective Properties [See Table 4-10]

Gaps in Model Gap Between Bottom Cover Plate 201 Air and Bottom End Plate Gaps in Grapple Region 202 Air Gap between the DSC and the TC bottom cover plateITC top cover plate 203 Air and also between the Top Flange and TC Top cover plate Gap between the DSCITC Annulus 206 Air Gap between Gamma Shield and 205 Air Structural Shell

Calculation No.: NUH32PHB-0402 Revision No.: 0 Page: 14of62 Table 4-4 Stainless Steel, SA 240, Type 304 / SA 182 Type F304N [6-8]

Temp P k Cp (OF) (Ib/in) (Btu/hr-in-°F) (Btu/Ib-°F) 70 0.717 0.114 100 0.725 0.114 200 0.775 0.119 300 0.817 0.122 400 0.867 0.126 500 0.290 0.908 0.128 600 0.942 0.130 700 0.983 0.132 800 1.017 0.132 900 1.058 0.134 1,000 1.100 0.136 Table 4-5 Carbon Steel, SA 516, Gr.70 [7, 9]

Temp P k Cp (OF) (Ib/in 3 ) (Btu/hr-in-°F) (Btu/Ib-°F) 70 1.967 0.106 100 1.992 0.110 200 2.033 0.118 300 2.033 0.122 400 2.017 0.128 500 0.284 1.975 0.133 600 1.925 0.136 700 1.867 0.143 800 1.808 0.148 900 1.742 0.155 1,000 1.667 0.164 Table 4-6 Gamma Shield, ASTM B29 Lead [5]

Temp p K CP (OF) (Ib/in 3) (Btu/hr-in-OF) (Btu/Ib-°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 0.030

81. 0.409 1.700 0.031 261 0.406 1.637 0.032 441 0.402 1.579 0.033 621 0.398 1.512 0.034

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 15 of 62 Table 4-7 Castable Neutron Shield, NS-3 [12, 15]

Operation Condition k C' Density 2 (lb/in3)

Normal & Fire Accident (Btu'in/hr-in -F) (Btu/Ibm-'F) 0.0407 0.145 0.0637 k Cp Density (Btu-in/hr'inZ'°F) (Btu/Ibm-'F) (lb/in)

Post-Fire Accident 0.0114 0.145 0.0605

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 16 of 62 Table 4-8 Air Thermal Properties [4]

Temperature Thermal conductivity Temperature Thermal conductivity (K) (W/m-K) (OF) (Btu/hr-in-°F) 200 0.01822 -100 0.0009 250 0.02228 -10 0.0011 300 0.02607 80 0.0013 400 0.03304 260 0.0016 500 0.03948 440 0.0019 600 0.04557 620 0.0022 800 0.05698 980 0.0027 1000 0.06721 1340 0.0032 The above data are calculated base on the tollowing polynomial function from [4].

k=

ZC, Ti for conductivity in(W/m-K) and T in (K)

For 250 < T < 1050 K CO -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 heat transfer coefficients in APPENDIX A based on the following data from [4].

c,== Ai T, for specific heat in (kJ/kg-K) and T in (K)

________________For 250< T < 1050 K AO 0.1 03409E+1 Al -0.2848870E-3 A2 0.781681 8E-6 A3 -0.4970786E-9 A4 0.1077024E-1 2 for viscosity (N-s/m 2)xl 06 and T in (K)

For250 < T < 600 K For600 < T < 1050 K B0 -9.8601E-1 BO 4.8856745 81 9.080125E-2 B1 5.43232E-2 B2 -1.17635575E-4 B2 -2.4261775E-5 B3 1.2349703E-7 B3 7.9306E-9 B4 -5.7971299E-11 B4 -1.10398E-12 p = P / RT for density (kg/m 3) with P=101.3 kPa; R = 0.287040 kJ/kg-K; T = air temp in (K)

Pr = cpu/k Prandtl number

A Calculation No.: NUH32PHB-0402 AREVA Calculation RevisionNo.: 0 TRANSNUCLEAR INC. Page: 17 of 62 Table 4-9 Helium Thermal Conductivity [4]

Temperature Thermal conductivity Temperature Thermal conductivity (K) (W/m-K) (OF) (gtulhr-in-°,F) 300 0.1499 80 0.0072 400 0.1795 260 0.0086 500 0.2115 440 0.0102 600 0.2466 620 0.0119 800 0.3073 980 0.0148 1000 0.3622 1340 0.0174 1050 0.3757 1430 0.0181 The above data are calculated base on the following polynomial function from [4]

k = -Ci Ti for conductivity in (W/m-K) and T in (K)

For 300 < T < 500 K for 500< T < 1050 K CO -7.761491E-03 CO -9.0656E-02 C1 8.66192033E-04 C1 9.37593087E-04 C2 -1.5559338E-06 C2 -9.13347535E-07 C3 1.40150565E-09 C3 5.55037072E-10 C4 0.OE+00 C4 -1.26457196E-13 Table 4-10 Thermal Properties of Homogenized Basket('1 ) [13]

Temp kbasnet rad Temp kbasket. axi Temp CD eff Pef (OF) (Btu/hr-in-°F) (OF) (Btu/hr-in-°F) (OF) (Btu/Ibm-°F) (lb/in4) 315 0.151 100 1.9946 70 0.095 403 0.160 200 2.0393 100 0.096 492 0.169 300 2.0760 200 0.098 581 0.179 400 2.1055 300 0.099 672 0.189 500 2.1160 400 0.100 0.131 763 0.199 600 2.1228 500 0.101 855 0.209 700 2.1297 600 0.101 949 0.218 800 2.1355 700 0.101 1045 0.224 900 2.1418 800 0.101 1143 0.227 1000 2.1474 900 0.102 1000 0.102 Note 1: See Appendix D for justification of effective density and specific heat.

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 18 of 62 Table 4-11 Effective Conductivity of Top Shield Plug and Top Cover Plate (See Section 5.4.1 for Justification)

Temp kradial k axial Cp_eff Peff (F) . (Btu/hr-in-0 F) (Btu/hr-in-°F) (Btu/Ibm-°F) (lb/in 3) 70 1.243 0.048 0.062 100 1.241 0.051 0.062 200 1.246 0.058 0.064 300 1.247 0.064 0.065 400 1.268(1" 0.071 0.067 500 1.254 0.077 0.068 0.352 600 1.250 0.083 0.068 700 1.249 0.088 0.069 800 1.245 0.094 0.069 900 1.244 0.099 0.070 1,000 1.244 0.104 0.071 Note: (1) 1.255 Btu/hr-in-0 F is conservatively used in the analysis Table 4-12 Effective Conductivity of Bottom Shield Plug (See Section 5.4.2 for Justification)

Temp kradial kaxial Cpeff Peff (OF) (Btu/hr-in-F) (Btu/hr-in-F) (Btu/Ibm-°F) (lb/in3) 70 1.362 0.062 0.053 100 1.358 0.065 0.053 200 1.352 0.074 0.054 300 1.345 0.082 0,055 400 1.358 0.090 0.056 500 1.332 0.098 0.057 0.367 600 1.320 0.105 0.057 700 1.309 0.112 0.058 800 1.297 0.119 0.058 900 1.286 0.126 0.058 1,000 1.276 0.132 0.059

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 19 of 62 Table 4-13 Effective Conductivity of Slide Rail (See Section 5.3 for Justification) trail = 0.12 in h contact = 2.7 Btu/hr-in 2-OF Temp k SS304 k eff (F) (Btu/hr-in-°F) (Btu/hr-in-0 F) 70 0.717 0.223 100 0.725 0.224 200 0.775 0.228 300 0.817 0.232 400 0.867 0.236 500 0.908 0.239 600 0.942 0.241 700 0.983 0.244 800 1.017 0.246 900 1.058 0.248 1000 1.100 0.250 4.4 Surface Properties of Materials The emissivity value of 0.587 is considered for both the DSC shell (stainless steel) and the transfer cask inner shell (stainless steel) in calculation of thermal radiation exchange between these shells [4].

It is assumed that the absorptivity and the emissivity of stainless steel are equal. Solar absorptivity 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 Criteria The 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 the temperature of the NS-3 solid neutron shielding material.

The melting point of ASTM B29 lead used in the gamma shield is approximately 620°F [8].

For design purposes of this application, the long-term, bulk average temperature of the NS-3 material is set to 280 OF [3] or less, and short-term limits for accident conditions should be 1,300 OF or less [17].

A Calculation No.: NUH32PHB-0402 AREVA Calculation RevisionNo.: 0 TRANSNUCLEAR INC. Page: 20 of 62 The design criteria and evaluation of 32PHB DSC basket for the various load cases shown in Table 4-1 are presented in Reference [13].

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 21 of 62 5.0 METHODOLOGY 5.1 CCNPP-FC TC Model A half-symmetric, three-dimensional finite element model of CCNPP-FC transfer cask (TC) is developed using ANSYS Version 10.0 [10] to provide the DSC shell temperature profile for 32PHB 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 end plates with a homogenized basket. The 32PHB DSC dimensions correspond to nominal dimensions listed in Table 4-2.

SOLID70 elements are used to model the components including the gaseous gaps. Surface elements SURF152 are used for applying the insolation boundary conditions. Radiation along the gap between DSC and TC inner shell is modeled using AUX12 processor with SHELL57 elements used to compute the form factors.

Decay heat load is applied as a uniform volumetric heat generated throughout the homogenized region of the basket. The volumetric heat generation rate is calculated as qM = 7r(Di Lb2

/2)2 Lb qm = 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 5-1 Table 5-1 Decay Heat Load DSC Type Heat Load Heat Load Di Lb Decay heat Load (kM) (Btu/hr) (in) (in) (Btu/hr-in 3) 32PHB 29.6 101004 66 158 0.1869 For load cases with insolance, the insolance is applied as a heat flux over the TC outer surfaces using average insolence values listed in Table 4-1. The insolance values are multiplied by the surface absorptivity factor to calculate the solar heat flux. The solar heat flux values used in CCNPP-FC TC model are summarized in Table 5-2.

A Calculation No.: NUH32PHB-0402 AR EVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 22 of 62 Table 5-2 Solar Heat Flux Operating Condition Solar Heat Flux Solar Total solar heat flux (Btu/hr-ft 2) Absorptivity (1) (Btu/hr-in 2)

Normal 82 0.587 (2) 0.334 Off-Normal/Accident 127 0.587 (2) 0.518 Note (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 together as total heat transfer coefficients. The total heat transfer coefficients are calculated using free convection correlations from Rohsenow Handbook [4] and are incorporated in the model using ANSYS macros. These correlations are described in APPENDIX A. The ANSYS macros 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 slide rails 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 this configuration shown in Figure 5-1, the distance between the centerline of DSC and centerline of the cask are calculated as follows.

R2 2 = R12 + x 2 - 2 R, x Cos(a)

With R, = Di, TC /2 - trail R2 = Do, DSC / 2 a = 18.50 x = Distance between the DSC and TC centerlines (See Table 5-3)

Di, TC = Inner diameter of TC (See Table 5-3)

Do, DSC = 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 shifted down 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 DiTC DoDSC R, R2 a x (in) (in) (in) (in) (degree) (in) 32PHB 68 67.25 33.88 33.625 18.5 0.27

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 23 of 62 The 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 TO model are shown in Figure 5-6 through Figure 5-7.

5.2 Fire Accident For 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 of 100 gallons of diesel fuel which is the maximum capacity of both fuel tanks within the tow vehicle is considered in Section 3.3.6 of CCNPP ISFSI USAR [3]. For this postulated fire accident with a conservative volume of 200 gallons of diesel fuel spill, the thickness of the fuel pool would be 1.63". This pool is assumed to burn at a minimum burning rate of 0.15 in/min

[18]. The 1.63" thick fuel pool would burn for 11 minutes. For conservatism a 15 minute fire duration is considered in this analysis.

To determine the maximum temperature of TC and DSC shell during the fire accident, a transient fire analysis is performed for duration of 15 minutes using the criteria described in 10CFR71, part 73 [1]. Based on the requirements in 10 CFR 71, part 73 [1], a fire temperature of 1475 OF and a conservative fire emissivity of 1.0 are considered for the fire conditions. Surface emissivity of 0.8 is considered for the packaging surfaces exposed to fire based on 10 CFR 71, part 73 [1]. A bounding forced convection coefficient of 4.5 Btu/hr-ft 2 -°F is 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 (See Table 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 of 1300OF +/- 100°F (50 minutes to get to 1300 0 F) for a period of one hour, the weight loss from NS-3 was 41 percent. A white smoke started to come out of the furnace at a temperature of 600'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 from Ref

[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 runs discussed in Section 6.0 show that the maximum temperatures of cask components except for 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 accident conditions.

The DSC shell temperature profiles from steady state runs will be used to determine the maximum basket component temperatures including the maximum fuel cladding temperature in a separate calculation [13].

Calculation No.: NUH32PHB-0402 Revision No.: 0 Page: 24 of 62 TC Ct R- = Di, TC /2 - trail R2 = D., DSC / 2 a = 18.50 DSC Ct R2 Slide Rail Figure 5-1 Location of 32PHB DSC within CCNPP-FC TC

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 25 of 62 Gamma Shield Cavity Gap Neutron Shield I /

Structural Shell TC Bottom NS-3 DSC End TC Top Cover TC Top NS-3 Plates Figure 5-2 Finite Element Model of CCNPP-FC TC with 32PHB DSC

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 26 of 62 Gamma Shield Cask Lid Ram/

Closure "I Plate Cask Inner Liner DSC Bottom Plates Figure 5-3 CCNPP-FC TC Finite Element Model, Components

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 27 of 62 0.0452" radial gap between structural shell and gamma shield 0.375" axial gap between the basket and DSC end plates 0.06" Axial Air Gap between the top flange 0.75" Radial Air Gap and TC top lid Air in the Grapple Region 0.5" Axial Air ,, 1 Gap between 0.75" Axial Air 0.025" radial the DSC and Gap between Air Gap TC bottom the DSC and between the TC top lid top flange and TC top lid Figure 5-4 Gaps in CCNPP-FC TC Model

A Calculation No.: NUH32PHB-0402 AREVA Calculation RevisionNo.: 0 TRANSNUCLEAR INC. Page: 28 of 62 Structural Shell

/

Annulus Neutron Shield Ribs 9 DSC Shell VJ-Gamma Shield Neutron Shield Inner Liner Horizontal TC (DSC is offset)

Figure 5-5 CCNPP-FC TC Finite Element Model, Cross Section

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 29 of 62 fN ELEMENTS HGEN RATES M*IN=0 QMAX=. 186854

• • r** - 0.02'0762

... - - ...... .. * * .04'1523

.062285

- _.... _ ** 083046 0

.03808

.12457

___ .145331

.166093

• .186854 Uniform Volumetric Heat Generation applied throughout Homogenized Basket Region Insolance Boundary Conditions Figure 5-6 Typical Decay Heat and Insolance Boundary Conditions

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 30 of 62 ANSYS 10.OAI OCT 5 2009 13:27:38 ELEMENTS PowerGraphics

'* EFACET=1 MAT' :NuN Xv, =630637 ZV *! 7 314,5 5,3.

• DIST=88.614 I Lr ,, *Xý: =23A.53

." *YF =-16 .313.

• ZF .=97.502 A-ZS=-3.O0O5 Z-BUFFER EDGE CONV- HCOE

-505

-504 m.-503

_-- -502

-501 Figure 5-7 Typical Convection and Radiation Boundary Conditions

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 31 of 62 5.3 Effective Conductivity of Slide Rails When the TC is in the horizontal orientation, the DSC is supported by the two rails depicted in DWG # BGE-01-3002. Given the weight of a loaded DSC (i.e., > 100,000 Ibs) and the surface area of the rails (i.e., 3-inch wide x 167.50-inches long), the contact pressure between a loaded DSC and the rail is in excess of 99 lbs/in 2 (assuming contact with two rails).

The thermal resistance between the DSC and the canister rails is assumed to be approximately 2.7 Btu/hr-in2 -OF [per Curve 11, page 4-19, Ref. 5].

The effective conductivity for the rails is calculated based on the following equation and is shown in Table 4-13:

keff = tra/t 1 kr,,i hreýis tan ce where:

trail = Thickness of the Rail = 0.12" kraii = Conductivity of NITRONIC 60 Rails (Assumed to be SA240 Type 304, See Table 4-4) hresistance = Contact Resistance = 2.7 Btu/hr-in 2-OF 5.4 Effective Thermal Properties of DSC End Plates The 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 Plate The effective properties for the end plates at the top of the DSC are calculated based on the following dimensions Table 5-4 Thickness and Weights of the Top End Assembly See Table 1 of Reference [14]

Component Thickness Volume Weight Material

[in] [in 3] [Ib]

Inner Top Cover Plate 1.5 5,107 1,461 SA240 Type 304 Top Shield Plug 4 13,208 5,429(2) ASTM B29 Top Casing for Lead(1 ) 0.75 2,477 708(2) SA240 Type 304 Outer Top Cover Plate 1.25 4,245 1,214 SA240 Type 304 Note (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 as shown in Table 1 of Reference [14]. The effect on the effective properties due to these changes is negligible.

A Calculation No.: NUH32PHB-0402 AREVA Calculation RevisionNo.: 0 TRANSNUCLEAR INC. Page: 32 of 62 Effective 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 these components and adjacent plates.

The various end plates along with the 0.0625" axial gaps between them built up serial thermal resistances along the axial direction. The effective conductivity through the serial plates is:

k tpae t Pltae 1p t t,itcp + t sp + tc + to,cp + (n

• tgap )

efa ,= t,,p + t,d + t 'CP + n

• tgap 21- +-+ +/c ++

kp/aie ktcp ktsp ktc ko~cp kair,gap where:

titcp, ttsp, ttc1, 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, kcl, kotcp, kair = Thermal conductivity of inner top cover plate, top shield plug, top casing 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. The effective conductivity through the parallel plates is:

(kplate tplate) =kicp

• t.,p + k,,p

• t,sp + k,,

• tl!i+ k ,tcp* totp keff,adia/l = *

• tplate titcp + t UP + t'C1 + totcp where:

titcp, ttsp, ttc, totcp = thickness of inner top cover plate, top shield plug, top casing for lead and outer top cover plate, respectively (See Table 5-4).

kjtcp, ktsp, ktc, kotcp = Thermal conductivity of inner top cover plate, top shield plug, top casing for lead and outer top cover plate, respectively (See Table 5-4 for materials and Section 4.3 for thermal conductivities).

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

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 33 of 62 Effective Density The effective density of the end plates is calculated as follows:

Pef~ Pp.'aie

• Vptate Pitcp

• V'C + Pisp

• V. + pi.,

• V'C + P.p 01

• OC p70= lToa vl,, + pVc + Vc, + V.P where:

t1tcp, ttsp, ttcl, totcp = thickness of inner top cover plate, top shield plug, top casing for lead and outer top cover plate, respectively (See Table 5-4).

Vitcp, Vtcl, Votcp = Volume of inner top cover plate, top shield plug, top casing for lead and outer top cover plate, respectively (See Table 5-4).

Effective Specific Heat The effective specific heat for the end plates is calculated as follows:

Cpeff ZWpate

• CPplate = Witcp

• CPitcp + Wtsp

• cptsp + WC,

• CPtc, + WotVP

• CPotcp Wrota,, w, + w= + wVo + wo=

where:

Cpitcp, Cptcp, C Cpotcp = Specific Heat of inner top cover plate, top shield plug, top casing for lead and outer top cover plate, respectively (See Table 5-4 for materials and Section 4.3 for Cp values).

Wtcpp,W W W*,tcp = Density of inner top cover plate, top shield plug, top casing for lead and outer top cover plate, respectively (See Table 5-4).

A constant specific heat of 0.030 Btu/lb-°F 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 shown in Table 4-11.

5.4.2 Bottom Shield Plug Assembly The effective properties for the end plates at the bottom of the DSC are calculated based on the methodology described in Section 5.4.1 and the following dimensions

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 34 of 62 Table 5-5 Thickness and Weights of the Bottom End Assembly See Table I of Reference [141 Component Thickness Volume Weight Material

[in] [in 3] [Ib]

Inner Bottom Cover Plate 1.75" 6,216 1,778 SA240 Type 304 Bottom Shield Plug 4.25" 14,650 6,021 ASTM B29 1

Bottom Casing for Lead" ' 0.5" 1,623 464 SA240 Type 304 Note (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.

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 35 of 62 6.0 RESULTS AND DISCUSSION Due to the high decay heat load of 29.6 kW considered for the NUHOMS 32PHB system the transfer 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 transfer operations are established based on the transient thermal analyses performed for normal vertical transfer conditions (load case # 5, Table 4-1) and off-normal hot horizontal transfer conditions (load case # 6, Table 4-1). The time limit established for off-normal hot transfer conditions 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 steady state with 212°F water in the TC-DSC annulus and the cask is in vertical orientation (i.e. no credit is taken for heat transferred through the rail). At time t= 0, the water in the cask is assumed to be drained, and the cask closure is completed. The TC is assumed to be left inside the fuel building in the vertical position.

For the off-normal hot transient condition (load case # 6), at time = 0, the cask is assumed to be 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 be considered after sealing the DSC when the water in the TC/DSC annulus starts to be drained completely.

The NUHOMS 32PHB system has a provision for forced convection to improve the thermal performance of the system during horizontal transfer conditions and is to be used only as one possible recovery mode if the operational time limits determined for load case # 6 in Table 4-1 are exceeded. The thermal performance of the NUHOMS 32PHB system with forced air convection will be analyzed in a separate calculation. The forced air convection is not relied on 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 both the vertical transfer operations (load case # 5) and the off-normal hot horizontal transfer operations (load case # 6). Table 6-1 summarizes the maximum temperatures for the CCNPP-FC TC components and shows that the maximum component temperatures are below 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 and 32PHB 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.

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 36 of 62 Table 6-1 Maximum Temperatures of CCNPP-FC TC @ 29.6 kW, NO Forced Air Circulation Temperature ['F]

Component Vertical Hot Off-Normal Hot Max. Allowable Load Case # 5 Load Case # 6 time = 20 hr Max. DSC Shell 1 395 407 ---

Inner Shell 279 313 ---

Gamma Shield 277 308 620 [8]

Structural Shell 242 263 ---

Bulk Avg. Temp of 280 [3]

Radial Neutron Shield 201 214 Bulk Avg. Temp of Top Neutron Shield Bulk Avg. Temp of 280 [3]

Bottom Neutron Shield 240 201 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 Figure 5-3 and does 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 15 minute fire. Figure 6-7 and Figure 6-8 show the temperature profiles for the steady state post-fire conditions. Table 6-2 presents the maximum component temperature at the end of 15 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 and Homogenized Basket during the fire and post-fire conditions. As seen from the figure and Table 6-2, the TC component, the DSC shell and basket temperatures are increasing during the 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 and neutron shield.

Figure 6-10 shows the bulk average temperature history of the NS-3 neutron shield in the TC during and after the fire accident. As seen from the Figure 6-10 the bulk average temperatures of the NS-3 components in the TC increase during the fire and their maximum temperatures are attained at the end of the fire and are listed in Table 6-2.

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 37 of 62 Table 6-2 Maximum Temperatures of CCNPP-FC TC for Accident Conditions Temperature [OF]

Fire Accident Component (15 Min. End of Post-Fire @Fire 48 Hours Post-Fire Steady State Max. Allowable Fire) Fire)after Max. DSC Shell (" 408 565 656 Inner Shell 307 492 590 ---

Gamma Shield 415 487 585 620 [8]

Structural Shell 352 447 568 ---

Bulk Rdl Avg. Temp of Neutron 542 295 359 1300 [17]

Radial Neutron Shield BulkAvg. Temp of 640 231 258 1300 [17]

Top Neutron Shield Bulk Avg. Temp of 441 258 291 1300 [17]

Bottom Neutron Shield Cask 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 and does not include the top and bottom end plates.

The maximum thermal stresses for the TC components except for the bottom cover plate and the ram access penetration ring occur during the hot ambient conditions as noted in Table 4.1.2.1 of [20]. Further the maximum stresses for the bottom cover plate and ram access penetration ring during the cold ambient conditions are significantly below the allowable stress limits. Therefore, the temperature gradients determined for the load case # 6 (Table 4-1, off-normal horizontal hot transfer conditions) are acceptable for the structural evaluation of thermal stresses for the CCNPP-FC TC with 32PHB DSC.

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 38 of 62 AN ocr 21 2009 18:33:36 PLOT NO. 4 NODAL SOLUTION TIME=20 TEMP SMN =162.269 SMX =278.741 162.269 175.21

' 188.152 201.093 rn 214.034

- 226.975

- 239.917 252.858 I 265.799 278.741 OtNEP-FC-TC with 32PHB, 29.6 kW- Vertical in Fuel Bldg Transient AN OCT 21 2009 18:33:34 PLOT NO. 3 NODAL SOLUTION TIME=20 TEMP SMN =162.269 SMXI162.269

=278.741 i

• 175.21

- 188.152 201.093 214.034 226.975

-- 239.917 252.858 265.799 278.741 cCNPP-FC-TC with 32PHB, 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)

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 39 of 62 AN OCT 21 2009 18:33:34 PLOT NO. 2 NODAL SOLUTION TnŽE=20 SMN =325.719 SMX mmm =440.551 325. 719

• 338.478 li

• 351.237

__ 363.996 376.755

• 389.514

• j

• 402.273

• ~415. 033

~427.792 440. 551 CCNPP-FC-TC with 32PHB, 29.6 kW - Vertical in Fuel Bldg Transient AN OCr 21 2009 18:33:33 PLOT NO. 1 NODAL SOLUTION TDIE=20 SMN =325. 719 N*!!

}

• i* SAK* =440.551 325. 719 Z),!*

• 351.237 363. 996 m389.514 m402.273 S415.033 440.551 oCNPF-FC-WC with 322HB, 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, 1000 F Ambient (load case # 5)

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 40 of 62 AM OCT 21 2009 18:28:23 PLOT NO. 4 NODAL SOLUTION TIME=20 T*MP SMN =163.456 SMX =313.262 163.456 180.101 196.746 213.391 230.037 246.682 F-]263.327 279.972 S296.617 313.262

=C-PP-FC-TC with 32PHB, 29.6 kW - Off-Normal Transfer Transient Runs AN OCT 21 2009 18:28:22 PLOT NO. 3 NODAL SOLUTION TIME=20 TEMP SMN =163.456 SNX =313.262 163.456 M 180.101 196.746 213.391 F-]246.682 263.327 279.972 296.617 313.262 OT-PP-FC-TC with 32PHB, 29.6 kW - Off-Normsal Transfer Transient Rins Figure 6-3 TC Temperature Distribution - Off-Normal Hot Transient, t = 20 hr

@ 29.6 kW, 127 Btu/hr-ft 2 Insolation, 104°F Ambient (load case # 6)

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 41 of 62 MY OCT 21 2009 18:28:22 PLOT NO. 2 NODAL SOUJTION TIME=20 SMN =265.733

• ii'*,:

SM =432.393 265 .733

• 284.25 302. 768

__321.286 F--'l 358. 322 I 376. 839 i

• 395.351 413. 875 432.393 CCNPF-FC-TC with 32PHB, 29.6 kW Off-Normal Transfer Transient Runs AN OCT 21 2009 18:28:22 PLOT NO. 1 NODAL SOLUTION TI*E=20 TEDP sT =265.733 SM =432.393 265.733 284.25

~321. 302.768 286 H, 339.804 H 358.322 376.839 395.357 F, 413.875 432.393 CXNPF-FC-TC with 32PHB, 29.6 kW - Off-Norml Transfer Transient Rins Figure 6-4 DSC Shell Temperature Distribution - Off-Normal Hot Transient, t = 20 hr

@ 29.6 kW, 127 Btu/hr-ft 2 Insolation, 104 0 F Ambient (load case # 6)

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 42 of 62 AN OCT 21 2009 18:44:53 PLOT NO. 2 NODAL SOLUTION STEP=-6 SUB =1 TIME=. 25 TEMP SMN =282.039 SMD=433.465 282.039 298. 864

[- 315. 689 4332.514 349.339

["7366. 165 F-q382.99 399. 815 416.64 433. 465 XCNPP-FC-TC with 32PHB, 29.6 kW - 15 Minute Fire Transient Runs AN OCT 21 2009 18:44:53 PLOT NO. 1 NODAL SOUJTION STEP=6 SUB =1 TIDE=. 25 SMN =282.039 SMv=433.465 282. 039 298.864 315. 689 332.514 349. 339 F-q366.165 F-q382.99 399. 815 416.64 F-1433. 465 CNFPP-FC-TC with 32PHB, 29.6 kW - 15 Minute Fire Transient Runs Figure 6-5 DSC Temperature Distribution - Fire Accident, t = 15 min.

@ 29.6 kW, 104 0 F Ambient (load case # 7)

A Calculation No.: NUH32PHB-0402 AREVA Calculation C

• Revision No.: 0 TRANSNUCLEAR INC. Page: 43 of 62 AN OCT 21 2009 18:44:54 PLOT NO. 4 NODAL STEP=-6SOLUTION SUB =1 TIME=.25 TEVFP SNN =198.825 SMX =1372 198.825 329.133 459.44 589.747 720.055 E- 850.362 980.669 iiii 1241 1372 GNPP-FC-TC with 32PHB, 29.6 kW - 15 Minute Fire Transient Runs AN OC 21 2009 18:44:53 PLOT NO. 3 NODAL SOLUTION STEP=-6 SUB =1 TIDE=. 25 SD'N =198.825 SMX =1372 198.825 329.133

[*459.44 589.747 720.055 850.362 980.669 1241 1372 CCNPP-FC-TC with 32PHB, 29.6 kW - 15 Minute Fire Transient umns Figure 6-6 TC Temperature Distribution - Fire Accident, t = 15 min.

@ 29.6 kW, 104'F Ambient (load case # 7)

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 44 of 62 AN OCT 21 2009 18:53:33 PLOTr NO. 4 NODAL SOLUTION STEP=-1 SUB =4 TIME=l SMN =166.088 SMX =590.332 166.088 213.226 260.364 307.502 354.64 401.779

- 448.917 496.055 543.193 590.332

=CNPP-FC-TC with 32PHB, 29.6 kW - Post Fire Steady State AN OCT 21 2009 18:53:32 PLCT NO. 3 NODAL SOLUTION STEP=-1 SUB =4 TINE=1 5*M =166.088 SMX =590.332 166.088 213.226 260.364 307.502 354.64 V-]401.119 V-]448.917 496.055 543.193 590.332 CCNPP-FC-TC with 32PHB, 29.6 kW - Post Fire Steady State Figure 6-7 TC Temperature Distribution - Post-Fire Accident, Steady State

@ 29.6 kW, 127 Btu/hr-ft2 , 104 0F Ambient (load case # 7)

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 45 of 62 AN CT 21 2009 18:53:32 PLOT NO. 2 NODAL SOLUTION STEP=-1 SUB =4 TI4E=1 SIVI =437.138 SDIX =692.066 437.138 465.463 493.789 522.114 550. 439 578. 765 635. 415 663. 741 692.066 CCNPP-FC-TC with 32PHB, 29.6 kW Post Fire Steady State AN OCT 21 2009 18:53:31 PI..OT NO. 1 NODAL SOLUTION STEP=-1 SUB =4 TINE=1 TEMP SMN =437.138 SME=692.066 437.138 M 465.463 493. 789 522.114 550. 439 578.765 b-- 607.09 635.415 F_1663.741 692.066 CXNPP-FC-TC with 32PHB, 29.6 kW - Post Fire Steady State Figure 6-8 DSC Shell Temperature Distribution - Post-Fire Accident, Steady State

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

Calculation No.: NUH32PHB-0402 Revision No.: 0 Page: 46 of 62 1400 1200 U_1000

• 800 E

0n

• VV 400 200

-2 8 18 28 38 48 Time [hr]

Figure 6-9 Temperature History for Fire and Post-Fire Conditions

@ 29.6 kW, 104'F Ambient (load case # 7)

Calculation No.: NUH32PHB-0402 Revision No.: 0 Page: 47 of 62 750 650

'- 550 1,.

a,_

0. 450 E-3 I.350 250 150

-2 8 18 28 38 48 Time [hr]

Figure 6-10 Bulk Average Temperature History of NS-3 in TC for Fire and Post-Fire Conditions @ 29.6 kW, 104 0 F Ambient (load case # 7)

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 48 of 62

7.0 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 can be left in the fuel building in a vertical orientation once the water in the DSC/TC annulus is drained. 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 shell for 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 7-1 Maximum Temperatures of CCNPP-FC TC @ 29.6 kW, NO Forced Air Circulation Temperature [OF]

Vertical Hot Off-Normal Hot Component Load Case # 5 Load Case # 6 (2) Max. Allowable time 20 hr Max. DSC Shell (1) 395 407 ---

Inner Shell 279 313 ---

Gamma Shield 277 308 620 [8]

Structural Shell 242 263 Bulk Avg. Temp of Radial Neutron Shield 201 214 280 [3]

Bulk Avg. Temp of Top Neutron Shield Bulk Avg. Temp of Bottom Neutron Shield 240 201 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 Figure 5-3 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

1. 6 (off-normal hot horizontal transient transfer operations).

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

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 49 of 62 Table 7-2 Maximum Temperatures of CCNPP-FC TC for Accident Conditions Components TimeTeprue Maximum 0 ]Jf Max. Allowable Temperature [OF] [OF]

Max. DSC Shell (1) 656 ---

Inner Shell oo 590 ---

Gamma Shield 0 585 620 [81 Structural Shell ,o 568 ---

Bulk Avg. Temp of Radial Neutron Shield End of Fire 542 1300 [17]

Bulk Avg. Temp of End of Fire 640 1300 [17]

Top Neutron Shield Bulk Avg. Temp of End of Fire 441 1300 [17)

Bottom Neutron Shield Cask Lid End of Fire 910 ---

Cask 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 and does not include the top and bottom end plates.

As seen the above tables, all design criteria specified in Section 4.5 are herein satisfied.

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 50 of 62 8.0 LISTING OF COMPUTER FILES All the runs 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".

A list of the files to create the finite element model of CCNPP-FC with 32PHB DSC is shown in Table 8-1.

Table 8-1 List of Geometry Files

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 51 of 62 A summary of ANSYS runs is shown in Table 8-2.

Table 8-2 Summary of ANSYS Runs Date / Time for Run Name Description Output File Initial conditions of the CCNPP-FC TC with 32PHB 10/21/2009 DSC in vertical orientation. 6:16 PM Off-normal hot horizontal transient transfer of the 10/21/2009 32PHBTOOFN_TRANS CCNPP-FC TC with 32PHB DSC 6:28 PM Vertical transient transfer of the CCNPP-FC TC 10/21/2009 32PHBTOVERT_TRANS with 32PHB DSC inside the Fuel Building 6:33 PM 10/21/2009 Initial conditions for the fire accident analysis 6:38/PM 32PHBTCOACCFIREINITIAL 6:38 PM 10/21/2009 15 Minute Fire Accident Analysis 6:44 PM 32PHBTCOACCFIRE_15MIN 24 Hour Post-Fire analysis 10/21/2009 32PHBTCOACCOPF - 7:15 PM 10/21/2009 Post-Fire Steady State Analysis 6:53 PM 32PHBTCOACCNS Temperature profile of 32PHB DSC for off-normal 10/21/2009 32PHBTCOOFNTRANS_20hr Map 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 PM 32PHB TC VERTTRANS 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 PM Temperature profile of 32PHB DSC shell for post- 10/21/2009 32PHBTOACCNS Map fire steady state conditions 7:00 PM 32PHBTOOFNTRANSSENS Sensitivity analysis for effective density and 02/24/2010 specific heat changes 3:15 PM

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 52 of 62 ANSYS macros, and associated files used in this calculation are shown in Table 8-3.

Table 8-3 Associated Files and Macros File Name Description Date / Time HTOTHCL.MAC Total heat transfer coefficients for horizontal cylindrical surface 2/19/2009

- 12:37 PM HTOTVPL.MAC Total heat transfer coefficients for vertical flat surface 2/19/2009

/12:37PM HTOTVCL.MAC Total heat transfer coefficients for vertical cylindrical surface 2/19/2009 9/3:52 PM HTOTFIRE.MAC Total heat transfer coefficients for fire 9/12/2008 118:33 PM 10/21/2009 32PHBTC Mat.inp - Material properties for CCNPP-FC Cask 6:07 PM 32PHBTC Mat3.inp Material properties for CCNPP-FC Cask for post-fire steady 10/21/2009 P astate 6:12 PM 32PHBTC PP.inp 9/16/2009 4:16 PM 32PHBTCOPPVERT.inp 9/16/2009

_ Marosfor5:48.ip

_ PM Macros for Post-Processing Transient Runs 9/16200 32PHB6TCOPPFIRE.inp 9/16/2009 6:48 PM 32PHBTCOPPPF.inp 9/22/2009 5:17 PM GammaGap_32PHB-TC.xls Spreadsheet to Calculate gamma shield/structural shell gap 01/27/2010 10:17 AM Gamma Gap_32PHB-TC-2.xls Spreadsheet to Calculate gamma shield/structural shell gap 01/27/2010 for post-fire steady state conditions 10:17 AM CCNPP-FC TC-Material Prop.xls Spreadsheet for material properties used in the analysis 9/21/2009 1:41 PM Fire History.xls Spreadsheet for Fire Temperature History Post Processing 10/27/2009 9:59 AM Macro for Creating Radiation Exchange between the DSC/TC 10/21/2009 32PHBTORAD_Horizontal.inp when the TC is in Horizontal Orientation 4:46 PM 32PHB TC RAIDVertical.inp Macro for Creating Radiation Exchange between the DSC/TC 10/21/2009 when the TC is in Vertical Orientation 4:42 PM

A Calculation No.: NUH32PHB-0402 AREVA Calculation RevisionNo.: 0 TRANSNUCLEAR INC. Page: 53 of 62 APPENDIX A TOTAL HEAT TRANSFER COEFFICIENTS Total heat transfer coefficient, ht, is used to combine the convection and radiation heat transfer together.

ht = hr + hc

Where, hr = radiation heat transfer coefficient (Btu/hr-in 2-IF) hc= free convection heat transfer coefficient (Btu/hr-in 2 _oF)

The radiation heat transfer coefficient, hr, is given by the equation:

hr (T,, - Tamb) = c F12 [ '(T.,4 - Trýmb) ]

h, = e F12 0-T-.b Btu/hr-in 2 "OF

~l2[ - Tamb

Where, 6 = surface emissivity F12 = view factor from surface 14 to ambient = 1 2

a = 0.1714 xl08 Btu/hr-ft -OR Tw = 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 free convection coefficients.

Horizontal Cylinders:

T.)D Ra=GrPr ; Gr= g 8 (T, S2f

=n(u + 2f /Nu T) with NUT =0.772 C, Ra1 / 4 f =1_ 0.13 with C=0.515 for gases [4]

Nut =C Ral 3 Ct =0.103 for air with Pr; 0.71 [4]

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 54 of 62 Nu = [(Nu,)m +(Nu,) m- I m with m = 10 for 10-'° <Ra <107 h, NuD 2 2 D k (Multiply by 0.1761/144 to convert from W/m -K to Btu/hr-in -OF) with g = gravitational constant =9.81 (m/s 2 )

P3= 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:

3 Ra=GrPr ; Gr/g,6(Tw,-T.)L 2

V 2.0 ln(l + 2.0 / NuT) with NUT =* Ra1 / 4 with C, =0.515 forgases [4]

Nu =Cv f Ra1/3 /(1+1.4x109 Pr/Ra) with 0.13 Pr0 22 0 . 7 8 (Tw 1 )

= (1+ 0.61 Pr`8 )°42 f = 1.0 + 0 , Too Nu = [(Nu,)m +(Nut) m I/m with m=6 for 1<Ra <1012 hc = NuL k (Multiply by 0.1761/144 to convert from W/m 2-K to Btu/hr-in 2-°F) with g = gravitational constant =9.81 (m/s 2 )

P = expansion coefficient = 1/T (1/K)

T = absolute temperature (K) v = kinematic viscosity (m 2/s)

L = height of the vertical surface (m) k = air conductivity (W/m-K)

The above correlations are incorporated in ANSYS model via macro "HTOT_VPL.MAC" listed in Section 8.0.

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 55 of 62 Vertical Cylindrical Surfaces:

Ra = Gr Pr  ; Gr = g,8 (T, 2 T.)

Nujplt,, =2.0 with ln(1 + 2.0 / Nu T )

NU~T C, Ra 114 with C-= 0.515 for gases [4]

_ ____18/

Nu,'pt, with -1.8 LIDT Nu, =

ln(+N Plate Nu, =Cv f Ral/3/(1+1.4x10o Pr/Ra) with Cv 0.13 Pr0 22 f=1.0+0.078T.- 1 t (1+ 0.61 Pro81) 42 Nu =(Nu,)r +(Nut)'I1 with m=6 for 1<Ra <1012 hc Nu k (Multiply by 0.1761/144 to convert from W/m2 -K to Btu/hr-in 2-OF)

L with g = gravitational constant =9.81 (m/s 2)

P = expansion coefficient = 1/T (1/K)

T = absolute temperature (K) v = kinematic viscosity (m 2/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 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 56 of 62 APPENDIX 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 the differential 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 70 0 F.

• During the lead pour the TC body and lead are at 620 0 F.

" The inner diameter of the gamma shell (lead) is equal to the outer diameter of the TC inner shell at thermal equilibrium.

The average coefficients of thermal expansion for SA-240 Type 304, SA516 GR70 and lead are listed in Table B-1.

Table B-1 Thermal Expansion Coefficients Temperature SA240 Type 304 SA516 GR70 Temperature Lead (OF) cc a (OF) a (in/in-°F) [11] (in/in-°F) [11] (in/in-°F)

[11]

70 8.46E-06 5.42E-06 70 16.07 E-6 200 8.79E-06 5.89E-06 100 16.21 E-6 300 9.00E-06 6.26E-06 175 16.58 E-6 400 9.19E-06 6.61E-06 250 16.95 E-6 500 9.37E-06 6.91 E-06 325 17.54 E-6 600 9.53E-06 7.17E-06 440 18.50 E-6 700 9.69E-06 7.41 E-06 620 20.39 E-6 The density of lead as a function of temperature is listed in Table.

Table B-2 Density of Lead Temperature Density *11] Temperature Density (K) (kg/m ) (OF) (Ibm/in 100 11,520 -280 0.4162 150 11,470 -190 0.4144 200 11,430 -100 0.4129 250 11,380 -10 0.4111 300 11,330 80 0.4093 400 11,230 260 0.4057 500 11,130 440 0.4021 600 11,010 620 0.3978

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 57 of 62 The volume within the "lead cavity" is found by determining the cask body dimensions at 620 0 F. As no gaps will be present between the molten lead and the cask body, this volume is also equal to the volume of lead at 620 0 F. The mass of the lead that fills the lead cavity at 620°F is then determined.

The dimensions of the "lead cavity" are calculated based on cask body temperature. A temperature of 305°F is considered for the cask body. This temperature is lower than the maximum cask inner shell temperature shown in Table 6-1. Since the gap size increases at lower temperatures, the above chosen value is conservative. From the mass of the lead and its density at 3051F, the lead volume is determined.

The length of the gamma shield at the TC body temperature is calculated based on thermal expansion coefficients listed in Table B-1. The lead volume is used to determine the maximum 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 Mass (XSS304, 620 = 9.56 x 10-6 in/in-°F at 620°F (via linear interpolation, Table B-1) o(CS516, 620 = 7.22 x 10-6 in/in- 0 F at 620°F (via linear interpolation, Table B-i)

Plead, 620 = 0.3978 Ibm/in 3 at 620°F (Table B-2)

Rin = inner radius of lead cavity at 70'F= 34.75" Rout = outer radius of lead cavity at 701F = 38.75" Lcavity = length of lead cavity at 70°F = 165.50" ain, 620 = (Rin)(1 +(a SS304, 6 20 )(AT)) = 34.9328" Rout, 620 = (Rout)(1 +((a cs516, 62 0)(AT)) = 38.9038" Lcavity, 620 = (Lcavity)(1 +(a cS516, 62 0)(AT)) = 166.1570" 2 2 Vcavity = Vlead, 620 = (7c)(Rout, 62 0 - Rin,620 )(Lcavity, 620) =

153,055.5 in3 Mlead = (Vlead, 620)(Plead, 620) = 60,878.5 Ibm Determination of Lead Gap cSS304, 305 = 9.01 x 106 in/in-OF at 305°F (via linear interpolation, Table B-i)

OCCS516, 305 = 6.28 x 10.6 in/in-°F at 305°F (via linear interpolation, Table B-I)

Clead, 620 = 20.39 x 10-6 in/in-°F at 6200F (via linear interpolation, Table B-i) cXlead, 305 = 17.38 x 10-6 in/in-°F at 305°F (via linear interpolation, Table B-1)

Plead,305 = 0.4048 Ibm/in 3 at 305OF (via linear interpolation from Table B-2)

Rin, SS304, 305 = (Rin)(1 +(oss304, 305)(AT)) = 34.8236" Rout, cS516, 305 = (Rout)(1 +(cX cs516, 305)(AT)) = 38.8072"

A Calculation No.: NUH32PHB-0402 AREVA Calculation RevisionNo.: 0 TRANSNUCLEAR INC. Page: 58 of 62 6 2 3 Llead, 305 = (Lcavity, 620)/[1 +((X lead,620)( 0- 70)]*(1 +(oc lead,305)( 05 - 70))

= 164.9855" Vlead, 305 = Mlead / Plead, 305 = 150,391.8 in3 Since Rin,SS 3 04 , 305 = Rin, lead, 305, then 2 2 )Led35 Vlead,305 = (i)(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 a gap 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 state analysis based on a temperature of 590°F for the cask body. This temperature is the maximum cask inner shell temperature shown in Table 6-2. The computed air gap between the lead and the structural shell is 0.004". To account for the effect in the reduction of the computed air gap between the gamma shield and structural shell from 0.0412" to 0.004", the effective conductivity of air in the region is increased by a factor of 4. This factor of 4 corresponds to an air gap of 0.011" (0.0452/4 = 0.0113") and is therefore conservative for the post-fire steady state conditions.

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 59 of 62 APPENDIX C DSC SHELL TEMPERATURE During the handling and vacuum drying operations, the DSC outer shell is in contact with water in annulus between the DSC and the transfer cask. The annulus is open to atmospheric pressure.

To bound the problem, it can be assumed conservatively that the total heat load from the assemblies flows to water in the annulus and no heat dissipation to ambient occurs. As long as the DSC shell is in contact with water, the decay heat will be used to evaporate and eventually boil the water in annulus. The water bulk temperature remains constant at 212°F (1000C) if water starts to boil.

The following calculation shows that the maximum allowable heat load for 32PHB DSC (29.6 kW [11]) is not adequate to boil the water in annulus. Therefore, the maximum bulk temperature 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, page 15.9]. The temperature gradient between the hot surface and the boiling water is defined as ATsat.

ATsat. = (Tw - Tsat) > 10 to 150C (C.1)

Tw = hot surface temperature (0c)

Tsat = saturated water temperature = 1000C at atmospheric pressure Under boiling water conditions, ATsat can be calculated using the following correlation from [4, page 15.46].

- 0.33 AT,., = Cs qDsc "i9g (C.2)

PLi'~'g g , g CSF = liquid/surface constant = 0.013 [4]

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

Jig = latent heat of vaporization = 970.3 Btu/lbm [4] = 2.257E6 J/kg a = surface tension of water = 0.059 N/M [4]

g = gravity constant = 9.8 m/s 2 [4]

p= density of saturated water = 958 kg/mi3 (vI = 1.0435E-3 m3/kg [19])

pg density of saturated steam= 0.598 kg/m 3 (Vg = 1.673 m3/kg [19])

k= conductivity of saturated water = 0.68 W/m-K [4]

All the properties are at 1000C.

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 60 of 62 The heat flux from DSC outer shell (qDsC") is calculated as follows.

_ Q _

qDsc" ( -Q - 1320 W/m 2 (C.3)

Q = maximum heat load per DSC = 29.6 kW [11]

ODDsc = Outer DSC shell diameter = 67.25" [11] = 1.708 m Lann = water height in annulus = DSC height -12" = 176.50 [14, Drawing NUH32PHB-30-1]-12"

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

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

ATsatann = 2.1CC (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 transfer cask.

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 61 of 62 APPENDIX D SENSITIVITY OF THE EFFECTIVE DENSITY AND SPECIFIC HEAT OF THE HOMOGENIZED BASKET This section presents a sensitivity analysis of the maximum temperatures in the CCNPP-FC TC to the changes in the effective density and specific heat of the homogenized basket considered in the transient analysis.

During the design process of the 32PHB DSC system, the weight of the fuel assembly is decreased which affects the effective specific heat and density of the homogenized basket considered in this calculation and shown in Table 4-10. The updated effective specific heat and density of the homogenized basket used in this appendix from [13] are listed in Table D-1.

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

Ternp Cp eff - Peff (JF) (Btu/Ibm-°F) (lb/in')

70 0.097 100 0.097 200 0.099 300 0.101 400 0.102 500 0.102 600 0.103 700 0.103 800 0.103 900 0.103 1000 0.104 Table D-2 presents a comparison on the maximum temperatures using the effective specific heat 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 1°F and is negligible. Therefore, the CCNPP-FC TC analysis and the resulting DSC temperature profiles used in the 32PHB DSC/Basket analysis in [13] for the fuel cladding temperatures remain bounding.

A Calculation No.: NUH32PHB-0402 AREVA Calculation Revision No.: 0 TRANSNUCLEAR INC. Page: 62 of 62 Table D-2 Sensitivity of Maximum Temperatures to Effective Density and Specific Heat Temperature [OF]

Component Off-Normal Hot Load Case # 6) Difference (Original Model, (Sensitivity Run) Table 6-1) Tsensitivity - Toriginal time = 20 hr Max. DSC Shell 408 407 +1 Inner Shell 314 313 +1 Gamma Shield 308 308 0 Structural Shell 264 263 +1 Bulk Avg. Temp of Radial Neutron Shield Bulk Avg. Temp of Top Neutron Shield Bulk Avg. Temp of Bottom Neutron Shield Cask Lid 217 216 +1 Cask Outer Shell 233 233 0