Revision as of 04:10, 11 October 2018

Text

NUH32PHB-0402, Revision 1, Thermal Evaluation of Nuhoms 32PHB Transfer Cask for Normal, Off-Normal, and Accident Conditions
	ML15075A344
Person / Time
Site:	Calvert Cliffs
Issue date:	03/10/2015
From:	; AREVA
To:	; Office of Nuclear Material Safety and Safeguards
Shared Package
ML15075A350	List: ML15075A339; ML15075A340; ML15075A341; ML15075A342; ML15075A344; ML15075A345; ML15075A346; ML15075A347; ML15075A348; ML15075A349;
References
	NUH32PHB-0402, Rev. 1
	Download: ML15075A344 (66)
	v • d • e

ENCLOSURE8 NUH32PHB-0402, Revision 1, Thermal Evaluation of NUHOMS 32PHB Transfer Cask for Normal, Off-Normal, and Accident Conditions Calvert Cliffs Nuclear Power Plant March 10, 2015 CONTROLLED COPY E-281 Form 3.2-1 Calculation No.: NUH32PHB-0402 Calculation Cover Sheet Revision No.: I AR EVA Revision 8 Page: 1 of 65 DCR NO (if applicable):

NUH32PHB-01 8 PROJECT NAME: NUHOMS 32PHB System PROJECT NO: 10955 CLIENT: CENG -Calvert Cliff Nuclear 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 0i No 0 (explain below) Licensi ng 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 1OCFR72.48 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: QI Jianwei 2015.03.03 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,.Lyndhb',g.

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 Gidsh 2015.03.03 16:14:20 -05*00'Project Engineer Name and Signature:

Girish Patel 5a3e0 Date: I Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 2of65 REVISION

SUMMARY

AFFECTED AFFECTED REV. DESCRIPTION PAGES Computational 110 0 Initial Issue All All 1 Add sensitivity studies of the applying the solar heat Additional run load to the full circumference of the cask when transfer 1-4, 7-8,16- files marked in the horizontal orientation to address RAI 6-6 from 17, 50-52, with revision NRC. The temperature term Tj is corrected to T'in and 63-65 bars listed in Tables 4-8 and 4-9 in response to RAI 6-11 from NRC. Section 8.0 Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 3of65 TABLE OF CONTENTS Page 1 .0 P u rp o se .............................................................................................................................

6 2.0 References

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

7 3.0 Assumptions 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 Dimensions in the CCNPP-FC TC Model .................................................

11 4.3 Thermal 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 Thermal 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 Computer Files ..........................................................................................

50 APPENDIX A Total Heat Transfer Coefficients

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

53 APPENDIX B Gamma shield gap justification

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

56 APPENDIX C DSC Shell Temperature

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

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

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

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

63 Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 4 of 65 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 Air Therm al Properties

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

16 Table 4-9 Helium Thermal Conductivity

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

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

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

21 Table 5-2 Solar H eat 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 irculatio 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 irculatio n ..................................................................................................

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

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

49 Table 8-1 List of G eom 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 Table 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 H e a t ...................................................................................................................

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

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

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

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

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

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

28 Typical Decay Heat and Insolance Boundary Conditions

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

29 Typical Convection and Radiation Boundary Conditions

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

30 TC Temperature Distribution

-Vertical Loading Transient, t = 20 hr @29.6 kW, No Insolation, 100 0 F Ambient (load case # 5) ...............................

38 DSC Shell Temperature Distribution

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

39 TC Temperature Distribution

-Off-Normal Hot Transient, t = 20 hr @29.6 kW, 127 Btu/hr-ft2 Insolation, 104 0 F Ambient (load case # 6) ...............

40 DSC Shell Temperature Distribution

-Off-Normal Hot Transient, t = 20 hr@ 29.6 kW, 127 Btu/hr-ft2 Insolation, 104 0 F Ambient (load case # 6) ...........

41 DSC Temperature Distribution

-Fire Accident, t = 15 min. @ 29.6 kW, 104 0 F Am bient (load case # 7) ......................................................................

42 TC Temperature Distribution

-Fire Accident, t = 15 min. @ 29.6 kW, 104 0 F Am bient (load case # 7) ......................................................................

43 TC Temperature Distribution

-Post-Fire Accident, Steady State @ 29.6 2 o kW , 127 Btu/hr-ft2, 104 0 F Ambient (load case # 7) ........................................

44 DSC Shell Temperature Distribution

-Post-Fire Accident, Steady State@ 29.6 kW, 127 Btu/hr-ft2, 104 0 F Ambient (load case # 7) ..........................

45 Temperature History for Fire and Post-Fire Conditions

@ 29.6 kW, 104 0 F A m bient (load case # 7) ...............................................................................

46 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 Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 6of65 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].

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 7 of 65

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 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 and Transfer Conditions", Transnuclear, Inc., NUH32PHB-0403, Rev.1.14 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.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 8of65 16 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", SANDIA Report, SAND 85-0196, TTC-0659, 1987.19 Weast, Astle, "CRC Handbook of Chemistry and Physics", 6 1 st 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 General License Facility," NUREG 1536, Rev. 1.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 9 of 65 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.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 10 of 65 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.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 11 of 65 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 Ambient Case Operation Condition Description Notes Temperature Insolation Airflow[°F] [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 (3) -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 212°F 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.

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 0.00556 hours 3.306878e-5 weeks 7.61e-6 months 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.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 12of65 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(1)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.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 13of65 Table 4-3 List of Materials in the CCNPP-FC TC Model Component Mat # in ANSYS Model Material Transfer Cask Properties Bottom Cover Plate (1" 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 SA182 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) 113__STMB29 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 60 (Effective Properties used.See Section 5.3)DSC Properties DSC Shell 301 SA240 Type 304 DSC Bottom Shield Plug Assembly 302 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 plate/TC 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 I I Calculation No.: NUH32PHB-0402 Revision No.: 1 Page: 14 of 65 Table 4-4 Stainless Steel, SA 240, Type 304 / SA 182 Type F304N [6-8]Temp P k Cp (OF) (Ib/in 3) (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 rable 4-5 Carbon Steel, SA 516, Gr.70 [7, 9 Temp P 3 k Cp (OF) (Ib/in) (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 I Table 4-6 Gamma 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 0.030 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 Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 15of65 Table 4-7 Castable Neutron Shield, NS-3 [12, 15]Operation Condition k C" Density Normal & Fire Accident (Btu-in/hr-in -OF) (Btu/Ibm-'F)

-"(lb/in3)0.0407 0.145 0.0637 k C Density Post-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.: 1 AREVA Page: 16 of 65 Table 4-8 Air Thermal Properties

[4]Temperature Thermal conductivity Temperature Thermal conductivity (K) (W/m-K) (OF) (atu/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 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 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].cp =iAj 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 0.7816818E-6 A3 -0.4970786E-9 A4 0.1077024E-12 for viscosity (N-s/m2)xl06 and T in (K)I For 250 < T < 600 K B0 -9.8601E-1 B1 9.080125E-2 B2 -1.17635575E-4 B3 1.2349703E-7 B4 -5.7971299E-11 For600 < T < 1050 K B0 4.8856745 B1 5.43232E-2 B2 -2.4261775E-5 B3 7.9306E-9 B4 -1.10398E-12 p = P / RT for density (kg/m 3) with P=1 01.3 kPa; R = 0.287040 kJ/kg-K; T = air temp in (K)Pr =cp ýi/k Prandtl number Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 17 of 65 Table 4-9 Helium Thermal Conductivity

[4]Temperature Thermal conductivity Temperature Thermal conductivity (K) (W/m-K) (OF) (Btu/hr-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 Ine aDove oaaa are calculated based on from [4]k = -Ci T' for conductivity in (W/the following polynomial function I I rn-K) and T in (K)For_300 < T < 500 K for_500< T < 1050 K CO -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 4-10 Thermal 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')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 0.100 763 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 0.131 1000 0.102 Note 1: See Appendix D for justification of effective density and specific heat.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 18of65 Table 4-11 Effective Conductivity of Top Shield (See Section 5.4.1 for Justification)

Plug and Top Cover Plate Temp kradial k axial Cpeff Pef3 (OF) (Btu/hr-in-°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"' 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 Pe3 (OF) (Btu/hr-in-F) (Btu/hr-in-F) (Btu/Ibm-°F) (Ib/in)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 Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 19 of 65 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-°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 620OF [8].For design purposes of this application, the long-term, bulk average temperature of the NS-3 material is set to 280 IF [3] or less, and short-term limits for accident conditions should be 1,300 OF or less [17].

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

[13].

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 21 of 65 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 SURF1 52 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 Q;r(D,/2)2 Lb q' = 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 (kW) (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.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 22 of 65 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.R 2 2 R+ 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)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 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 Di,Tc Do,DSC R 1 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.: 1 AREVA Page: 23 of 65 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 TC 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-OF 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 0.00556 hours 3.306878e-5 weeks 7.61e-6 months 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 1300°F +/- 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 0.0133 hours 7.936508e-5 weeks 1.8264e-5 months 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.: 1 Page: 24 of 65 TC Ct a= 18.50 R0 = Di, TC /2 -trail R2 = Do. DSC / 2 R 1 DSC Ct Slide Rail Figure 5-1 Location of 32PHB DSC within CCNPP-FC TC Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 25 of 65 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 Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 26 of 65 Gamma Shield Cask Outer Shell Ram Cask Lid Closure Plate Cask Inner Liner DSC Bottom Plates\ t Figure 5-3 CCNPP-FC TC Finite Element Model, Components Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 27 of 65 0.0452" radial gap between structural shell and gamma shield 0.75" Radial Air Gap/0.375" axial gap between the basket and DSC end plates 0.06" Axial Air Gap between the top flange and TC top lid Air in the Grapple Region 0.5" Axial Air Gap between the DSC and TC bottom 0.75" Axial Air 0.025" radial Gap between Air Gap 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 Calculation Revision No.: 1 AREVA Page: 28 of 65 Structural Shell/DS6r I-'44 AnnulusDSC Shell Gamma Shield Neutron Shield Ribs MI Neutron Shield Inner Liner Horizontal TC (DSC is offset)CCNPP-FC TC Finite Element Model, Cross Section Figure 5-5 Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 29 of 65 AN ELEMENTS HGEN RATES QMIN=0 QMAX=. 186854 0.020762.041523.062285.083046-.103808 m .12457 L-- .145331-.166093 I .186854 ilied on Uniform Volumetric Heat Generation app throughout Homogenized Basket Regi Insolance Boundary Conditions Figure 6-6 Typical Decay Heat and Insolance Boundary Conditions Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 30 of 65 ANSYS 10.OAI OCT 5 2009 13:27:38 ELEMENTS PowerGraphics EFACET=1 MAT NUM XV =.630637 YV =.250458 zv =.734553*DIST=88.

614*XF =23.853*YF =-16.313*ZF =97.502 A-ZS=-3. 005 Z-EBUFFER EDGE CONV-HCOV m -5*05 3-504-503-502-501 Figure 5-7 Typical Convection and Radiation Boundary Conditions Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 31 of 65 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/in2 (assuming contact with two rails). The thermal resistance between the DSC and the canister rails is assumed to be approximately 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 is shown in Table 4-13: keff= ri trail 1 kra,1 hres tan ce where: 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-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') 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.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 32 of 65 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: atpte t,,c' +tsp +tI +ct!,p +(n* tK )keff.arial

-tplate titu ttsp to tticp *tgap E p t + + + t +kpate khi p ktsp k,.l k,,Cp a ..gap where: 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, 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: keg ff.a, X (kplae*tpte)

-k,,tp

t , ,'p + kp

t,,p + k,c,

tc, + ko,,p

t,,p kEff~ri tplate tcsps+ ptU + tl atp where: titcp, 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).kitcp, 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.

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

Vpia. ie,,cp

VCi +

VP + p,..

vKC, +

Vo..p eff VTo.o, V,,CP +v +,, ++/-V" +Vo, where: titcp,, 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).Vitcp,,, Vt, Vote = 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: CPef= Wpotw

Cpp,t= W_ tcp

Cpit 1 p + WtsP

Cpt,p + WMc,

Cptc, + Wotcp

Cp 0 cp eWTotW, W, 4 p + Wt.V + Wto, + where: Cptcp,, Cpt, Cptc, 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).Witcp, Wtsp, Wtcl, Wotcp = 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/Ib-0 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 Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 34 of 65 Table 5-5 Thickness and Weights of the Bottom End Assembly See Table 1 of Reference

[14]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 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.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 35 of 65 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 0.00556 hours 3.306878e-5 weeks 7.61e-6 months 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 0.00556 hours 3.306878e-5 weeks 7.61e-6 months .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 0.00556 hours 3.306878e-5 weeks 7.61e-6 months for the CCNPP-FC TC and 32PHB DSC.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 36 of 65 Table 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 # 6 time = 20 hr Max. DSC Shell " 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.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 0.0133 hours 7.936508e-5 weeks 1.8264e-5 months 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.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 37 of 65 Table 6-2 Maximum 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 Fire Fire)Max. DSC Shell (" 408 565 656 Inner 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 Shield Bulk Avg. Temp of 640 231 258 1300 [17]Top Neutron Shield BulkAvg. 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.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 38 of 65 AN OCT 21 2009 18: 33: 36 PLOT NO. 4 NOEDL SOIUTION TIME=20 STM =162.269 SM =278.741 m 162.269 m 15.21 188.152 201.093 214.034-226.975 239.917 252.858 265.799 278.741 OCMP-FC-TC with 32PHB, 29.6 kW -Vertical in Fuel Bldg Transient AN OCT 21 2009 18:33:34 PKDT NO. 3 NODAL SOIUTON TBF--20 TEMP SMN =162.269 SMK =278.741 m162.269 mm175.21 188.152 201. 093 mm214.034 226.975[-7239.917 m 252.858 m265.799 278.741 OCW-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.: 1 AREVA Page: 39 of 65 AN OCT 21 2009 18: 33: 34 PIwr NO. 2 NODAL SOLUTION TIME=20 TEMP SMt =325.719 SMX =440.551 325.719 338.478 351.237 363.996 376.755 389.514 402.273 415.033 427.792 440.551 CtWP-FC-TC with 32PHB, 29.6 kW -Vertical in Fuel Bldg Transient AN OCT 21 2009 18: 33: 33 PLT NO. 1 NODAL SOLUIMON TDhE=20 5MN =325.719 SK -=440.551 325. 719 338.478 351.237 363.996 376.755 389.514-402.273 415.033 427.792 440.551 (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.: 1 AREVA Page: 40 of 65 AN OCT 21 2009 18:28:23 PLOT NO. 4 NODAL SOITION TIbE=20 SMN =163.456 SM3 =313.262 163.456 180.101 196.746 213. 391 230.037 246.682 263.321 279.972 296.617 313.262 E'EP-FC-TC with 32PMB, 29.6 kW -Off-Normal Transfer Transient Runs AN OCT 21 2009 18:28:22 PLOT NO. 3 NODAL SOCLLION TIME=20 TEMP SMN =163.456 SM =313.262 163.456 180.101 196.746 213.391 230.037 246.682-263.327 279.972 296.617 313.262 OMIP- TC-' with 32PHB, 29.6 kW -Off-Normal Transfer Transient Puns Figure 6-3 TC Temperature Distribution

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

A Calculation No.: NUH32PHB-0402 Calculation Revision No.: 1 AREVA Page: 41 of 65 AN OCT 21 2009 18:28:22 PLOr NO. 2 NODA~L SOIIJTIOCI TIME=20 SM =265.733 SM =432.393 265.733 284.25mmm302.768 321.286 339.804 358.322_ 376.839-395.357 413.875 432.393 (CCWP-FC--C with 32PHB, 29.6 kW -Off--Normal Transfer Transient Rmns AN OCT 21 2009 18:28:22 PIDr NO. 1 NODAL SOLUTION TIhE=20 S1N =265.733 SMX =432.393 265.733-284.25 m 302.168 321.286 339.804 m m 358.322 m m 376.839 395.357 413.875 432.393 OUEP-FC--I with 32PB, 29.6 kW -Off-iormal Transfer Transient am Figure 6-4 DSC Shell Temperature Distribution

-Off-Normal Hot Transient, t -20 hr@ 29.6 kW, 127 Btulhr-ft 2 Insolation, 104 0 F Ambient (load case #6)

Calculation No.: NUH32PHB0402 A Calculation Revision No.: 1 AREVA Page: 42 of 65 AN OCT 21 2009 18:44:53 PI!r NO. 2 NODL SOUMOic.P=6 SUB =1 Tfl'E=. 25 SMN =282.039 SW =433.465 282.039 298.864 315.689332.514 349.339 EEZI366.165 EJ 382.99 399. 815 416.64 433.465 CflPP-FC-TC with 32FHB, 29.6 kW -15 Minute Fire Transient R=ns AN OCT 21 2009 18:44:53 PLOT NO. 1 NODL SOEL]rION STIEP=6 SUB =1 TIM--. 25 I N =282.039 SW =433.465 282.039 298.864 315.689 332.514 I 349.339 I__ 366.165 I 382.99399.815*416.64 433.465 C2NPP-FC-TI with 32PMB, 29.6 kW -15 Minute Fire Transient Rums Figure 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.: 1 AREVA Page: 43 of 65 AN OCr 21 2009 18:44:54 PIXr NO. 4 NODAL STEP=6 SUB =1 TIME=. 25 TEP S =198.825=1372 198.825 329.133 l 459.44 EM 589.747= 120.055 850.362 U-]980.669 iiii 1241 1372 CaFF=-FC-TC with 29.6 kW -15 Minute Fire 7Tansient R AN T 21 2009 18:44:53 PLOT NO. 3 NODAL SOIwrION SIEF=6 SUB =1 TIME=.25 TEMP MN =198.825 SM =1372 198.825 329.133 459.44 m 589.747 720.055 850.362_-- 980.669 1111 1241 1372 XCNPP-FC-WC with 32PHB, 29.6 kW -15 Minute Fire Transient Runs Figure 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.: 1 AREVA Page: 44 of 65 AN CT 21 2009 18:53:33 PIDr NO. 4 NODAL SOLUTION STEP=-1 SUB-=4 TIME=1 TEMW SMN =166.088 SM =590.332 166.088 213.226 260.364 307.502 m 354.64 401.779 448.917 496.055 543.193 590.332 CCNPP-FC-TC with 32PHB, 29.6 kW -Post Fire Steady State AN OCr 21 2009 18:53:32 P= NO. 3 NODAL SOU3TION STEP=-1 SUB--4 TBhE=1 TEMP SMN =166.088 SMX =590.332 m 166.088 m213.226 260.364 307.502 m 354.64 401.779_-_ 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-ft 2 , 104 0 F Ambient (load case # 7)

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 45 of 65 AN OCT 21 2009 18:53:32 PLOr NO. 2 NAL SOUTrION S7EP--1 SUB =4 TIME=1 S =437.138 SM =692.066 437.138 465.463 493.789 522.114 I. 550.439 E2I 578.765 I 607.09 635.415 663.741 692.066 MEFP-FC-TC with 32PHB, 29.6 kW -Post Fire Steady State AN Wr 21 2009 18:53:31 PLOT NO. 1 NOAL SOLUTI O TRIE,=1 S3N =437.138 SMK =692.066437.138~465. 463493.789522.114 550.439 578.765 607.09 635.415 692.066 CCNEP'-FC-TC with 32PFB, 29.6 kW -Post Fire Steady State Figure 6-8 DSC Shell Temperature Distribution

-Post-Fire Accident, Steady State@ 29.6 kW, 127 Btulhr-ft 2 , 104 0 F Ambient (load case # 7)

Calculation No.: NUH32PHB-0402 Revision No.: 1 Page: 46 of 65 1400 1200 4-0.u000 800 E 0! Basket-U-DSC Shell Inner Liner Gamma Shield-)K-Structural Shell-*-Outer Shell 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 0 F Ambient (load case # 7)

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 48 of 65

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 0.00556 hours 3.306878e-5 weeks 7.61e-6 months .Further a time limit of 20 hours2.314815e-4 days 0.00556 hours 3.306878e-5 weeks 7.61e-6 months 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 DSCITC 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 0.00556 hours 3.306878e-5 weeks 7.61e-6 months .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 232 186 280 [3]Bulk Avg. Temp of Bottom 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 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 #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.

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

~ I Ternperature

[°F] rOF]Max. DSC Shell c1 656 Inner 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 of T uto Shield End of Fire 640 1300 [17]Top Neutron Shield Bulk Avg. Temp of Bottom Neutron Shield End of Fire 441 1300 [17]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.

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 50 of 65 8.0 LISTING OF COMPUTER FILES All 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 version 10.0 [10] with operating system "RHEL5.6x64" on the AREVA HPC cluster with Intel X5675 CPUs.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 Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 51 of 65 A summary of ANSYS runs is shown in Table 8-2.Table 8-2 Summary of ANSYS Runs Date I 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 32PHBTCOFN_TRANS CCNPP-FC TC with 32PHB DSC 6:28 PM 32PHBTOVERTTRANS Vertical transient transfer of the CCNPP-FC TC 10/21/2009 with 32PHB DSC inside the Fuel Building 6:33 PM 10/21/2009 32PHBTCOACCFIREINITIAL Initial conditions for the fire accident analysis 6:38 PM 10/21/2009 32PHBTCOACCFIRE_15MIN 15 Minute Fire Accident Analysis 6:44 PM 10/21/2009 32PHBTCOACCPF 24 Hour Post-Fire analysis 7:15 PM 10/21/2009 32PHBTCOACCONS Post-Fire Steady State Analysis 6:53 PM 32PHB 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 0.00556 hours 3.306878e-5 weeks 7.61e-6 months 6:44 PM 32PHBTOVERTTRANS 20hr Map Temperature profile of 32PHB DSC for vertical 10/21/2009

---transient transfer conditions

@ 20 hours2.314815e-4 days 0.00556 hours 3.306878e-5 weeks 7.61e-6 months 6:49 PM 32PHBTOACO NS Map Temperature profile of 32PHB DSC shell for post- 10/21/2009 fire steady state conditions 7:00 PM 3Sensitivity analysis for effective density and 02/24/2010 32PHB TC OFNsTRANSpSENS specific heat changes 3:15 PM Off-normal hot horizontal transient transfer of the 01/20/2015 32PHB_TCOFN1_TRANS CCNPP-FC TC with 32PHB DSC ( solar heat load 11:38 AM applied 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 PM circumference)

Off-Normal Transfer Conditions

@ 20 hrs, 104 0 F 01/20/2015 32PHBOFN1 ambient, 29.6 kW (solar heat load applied on TC 3:30 PM full circumference)

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 52 of 65 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 I 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 12:37 PM HTOTVCL.MAC Total heat transfer coefficients for vertical cylindrical surface 2/19/2009-3:52 PM HTOTFIRE.MAC Total heat transfer coefficients for fire 9/12/2008 18:33 PM0 32PHBTCMat.inp Material properties for CCNPP-FC Cask 10/21/2009

-6:07 PMV 32PHBTC Mat3.inp Material properties for CCNPP-FC Cask for post-fire steady 10/21/2009 2astate 6:12 PM 32PHBTC PP.inp 9/16/2009 4:16 PM 32PHB_TC_PP1.inp 1/20/2015 11:38 AM 32PHBTCOPPVERT.inp Macros for Post-Processing Transient Runs 9/16/2009 5:48 PM 32PHBTCPPFIRE.inp 9/16/2009 6:48 PM 32PHBTCOPPPF.inp 9/22/2009 5:17 PM Gamma Gap_32PHB-TC.xls Spreadsheet to Calculate gamma shield/structural shell gap 01/27/2010 10:17 AM GammaGap_32PHB-TC-2.xls Spreadsheet to Calculate gamma shield/structural shell gap for 01/27/2010 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 RADVertical.inp Macro for Creating Radiation Exchange between the DSC/TC 10/21/2009 when the TC is in Vertical Orientation 4:42 PM 32PHB Model.db ANSYS Geometrical File for 32PHB DSC [211 32PHB Matl.inp Material properties for 32PHB DSC with Helium [21]32PHB HLZC2.MAC Heat generation for 32PHB DSC, 29.6 kW [211 Macro.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.: 1 AREVA Page: 53 of 65 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-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 F 1 .b 4) Btu/hr-in 2T-bF i[ Tu.. -Tainh Where, 6 = surface emissivity F 1 2 = view factor from surface 1 to ambient = 1 a = 0.1714 x10-8 Btu/hr-ft 2-OR 4 T, = 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:

Ra =Gr Pr ; Gr =g 8 (T,,,- T.) D V 2 2f N ln(1u+2fNu T) with N-T- 1 0.13 -Nu T =0.772 C, Ra 1 1 4 ; f=1 (NuT)0.16 with C, = 0.515 for gases [4]Nut C, Ra 1 3 Ct = 0.103 for air with Pr z, 0.71 [4]

Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 54 of 65 Nu = [(Nu,)- +(NU,)-I'mr with m=10 for 1010 <Ra <i10 k = Nu k (Multiply by 0.1761/144 to convert from W/m2 -K to Btu/hr-in2 -F)D with 2 g = 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?V 2 Nu, -2.0 ln(1 + 2.0 /Nu T) with NUT =5, Ra 1 4 with C, =0.515 forgases [4]Nu =Cv f Ra 13/(1+1.4x109 PriRa) with Cv = 0.13Pr 0 2 2 0.42 f =1 (1+ 0.61 Pro`8 1)4 2 f =T0 .Nu=[(Nu,)-

+(Nut)m-Im with m=6 for 1<Ra<10 1 2 hc = Nuk (Multiply by 0.1761/144 to convert from W/m2 -K to Btu/hr-in2 -F)L with g = 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" listed in Section 8.0.

Calculation No.: NUH32PHB-0402 ACalculation Revision No.: 1 AREVA Page: 55 of 65 Vertical Cylindrical Surfaces: Ra=GrPr ; Gr =g#(Tw -T.)L V 2 2.0 lIn(1 + 2.01 Nu T)Ra with C,=0.515 for gases [4]Nu with_ 1.8 LID Nupt = PlaRa UT Nu, -In(1 + 4) NuNpate with Pl at N ui pate Nut= Cv f Ra 13 /(1 + 1.4 x 109 Pr/Ra) with Cv= (1+0.61Pr 0.2 2 f = 1.0 + 0.078kT- --1 Nu=[(Nu,)m

+(NU,)n'mIn/

with m=6 for 1<Ra<10 1 2 hc = Nu-k (Multiply by 0.1761/144 to convert from W/m2 -K to Btu/hr-in2 -F)L with g = 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.: 1 AREVA Page: 56 of 65 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 701F.* 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-i.Table B-1 Thermal 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-06 200 8.79E-06 5.89E-06 300 9.OOE-06 6.26E-06 400 9.19E-06 6.61E-06 500 9.37E-06 6.91E-06 600 9.53E-06 7.17E-06 700 9.69E-06 7.41 E-06 Temperature Lead (OF) a (in/in-°F)

[11]70 16.07 E-6 100 16.21 E-6 175 16.58 E-6 250 16.95 E-6 325 17.54 E-6 440 18.50 E-6 620 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 ;1 1] Temperature Density (K) (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 Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 57 of 65 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 305 0 F, 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 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/in 3 at 620°F (Table B-2)Rin = inner radius of lead cavity at 70 0 F= 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, 6 2 0)(AT)) = 34.9328" Rout, 620 = (Rout)(1 +(C CS516, 6 2 o)(AT)) = 38.9038" Lcavity, 620 = (Lcavity)(1

+(C CS516, 6 2 0)(AT)) = 166.1570" Vcavity = Vlead, 620 = (7c)(Rout,62o2

-Rin, 6 2 0 2)(Lcavity, 620) = 153,055.5 in3 Mlead = (Vlead, 620)(Plead, 620) = 60,878.5 Ibm Determination of Lead Gap Xss3o4, 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/in 3 at 305°F (via linear interpolation from Table B-2)Rin,SS304, 305 = (Rin)(l+(ass304, 3 0 5)(AT)) = 34.8236" Rout, cS516, 305 = (Rout)(1 +(a CS516, 3 o 5)(AT)) = 38.8072" 4 A Calculation No.: NUH32PHB-0402 Calculation Revision No.: 1 AREVA Page: 58 of 65 Llead, 305 = (Lcavity, 620)/[1 +(c, lead,620)(6 2 0 -70)]*(1 +(a lead,305)(3 0 5 -70))= 164.9855" Vlead, 305 = Mlead / Plead, 305 = 150,391.8 in 3 Since Rin,SS 3 0 4 , 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 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.

Calculation No.: NUH32PHB-0402 Calculation Revision No.: 1 AREVA Page: 59 of 65 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 (1 00°C) 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 10-15 0 C 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)T, = 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_ il 1 i, 3 lg ,[-1 g (C.2)CSF = liquid/surface constant = 0.013 [4] 2 qDSC" = 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/m 2 [4]ilg = latent heat of vaporization

= 970.3 Btu/lbm [4] = 2.257E6 J/kg c = surface tension of water = 0.059 N/M [4]g = gravity constant = 9.8 m/s2 [4]p= density of saturated water = 958 kg/mi 3 (vI = 1.0435E-3 m 3/kg [19])Pg = density of saturated steam= 0.598 kg/mi 3 (Vg = 1.673 m 3/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.: 1 AREVA Page: 60 of 65 The heat flux from DSC outer shell (qDsc") is calculated as follows.qDSC" -OQ -1320W/m 2 (C.3);r OD 0 sc L.ann1 Q = maximum heat load per DSC = 29.6 kW [11]ODosc = 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.ATsatan. = 2.1°C (C.4)ATsat,ann is much lower than the required temperature gradient of 10 to 15 0 C 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 Calculation Revision No.: 1 AREVA Page: 61 of 65 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]Temp Cp eff eff (OF) (Btu/Ibm-°F) (lb/in*)70 0.097 100 0.097 200 0.099 300 0.101 400 0.102 0.126 500 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 1OF 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.

Calculation No.: NUH32PHB-0402 Revision No.: 1 Page: 62 of 65 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 Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 63 of 65 APPENDIX E SENSITIVITY STUDY OF APPLYING SOLAR HEAT LOAD TO FULL CIRCUMFERENCE OF THE CASK IN THE HORIZONTAL ORIENTATION The thermal evaluation methodology presented in Section 5.1 considers that the lower halves of the CCNPP-FC TC cylindrical surfaces are not exposed to insolance during outdoor transfer operations in horizontal orientation.

This evaluation considers a conservative solar heat load of 127 Btu/hr-ft2 for a 24 hour2.777778e-4 days 0.00667 hours 3.968254e-5 weeks 9.132e-6 months 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 surfaces and 200 gcal/cm for vertical flat surfaces over a 12 hour1.388889e-4 days 0.00333 hours 1.984127e-5 weeks 4.566e-6 months period.However, because of the large thermal inertia of the TC, the insolation values listed in 10 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 solar heat 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 for vertical flat surfaces.

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

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

2) (2) (Btu/hrft 2) (2)Curved Surface 400 61.4 127 Vertical Flat Surface 200 30.7 127 Note (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 the upper 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 areas of the TC using the insolation values from 10 CFR 71.71 [1]. The insolation values from 10 CFR 71.71 are averaged over 24 hours2.777778e-4 days 0.00667 hours 3.968254e-5 weeks 9.132e-6 months and multiplied by the surface absorptivity factor to calculate the solar heat flux. The total solar heat flux values applied in the sensitivity analysis are listed in Table E-2.

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

(1) (Btu/hr-ft

2) (3) Absorptivity (2) (Btu/hr-in 2)Curved Surface 400 61.4 0.587 0.250 Vertical Flat Surface 200 30.7 0.587 0.125 Note (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 Load Case # 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 the sensitivity 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, DSC components and TC components with solar heat load applied to the full circumference of the TC to the design basis values listed in Table 7-1 of this calculation and Table 6-1/Table 6-2 of [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 the full circumference) vary slightly compared to the design basis temperatures determined with a solar heat load 127 Btu/hr-ft (applied over the upper half of the curved surfaces and on all vertical surfaces).

However, all temperatures remain below their allowable limits and there is no adverse impact due to the application of solar heat load over the entire circumference of the TC outer surfaces.Further, as described in Section 5.1.2 of [21], thermal stress evaluation of the TC loaded with 32PHB DSC is based on design basis thermal stress evaluation of the TC loaded with 32P DSC, which is documented in [20]. As discussed in Section 3.4.1 of Appendix 1 in [20], the thermal stress analysis is based on a design temperature for the TC of 400 OF, which is higher 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 the fuel cladding due to the change in the solar heat load boundary conditions.

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

This shows that the fuel

-q Calculation No.: NUH32PHB-0402 A Calculation Revision No.: 1 AREVA Page: 65 of 65 cladding and DSC components are not impacted due to the change in the application of the solar heat load.Therefore, the application of the conservative solar heat load of 127 Btu/hr-ft2 only to the top half of the transfer cask during outdoor transfer operation is adequate to evaluate the thermal performance 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 DSC Temperature

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

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

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

ML15075A344: Difference between revisions

Revision as of 04:10, 11 October 2018

Contents

Text

SUMMARY

SUMMARY

2.0 REFERENCES

3.2 32PHB

4.2 Major

7.0 CONCLUSION

Navigation menu

ML15075A344: Difference between revisions

Revision as of 04:10, 11 October 2018

Text

SUMMARY

SUMMARY

2.0 REFERENCES

3.2 32PHB

4.2 Major

7.0 CONCLUSION

Navigation menu

Search