ML20212N423
| ML20212N423 | |
| Person / Time | |
|---|---|
| Site: | 07109071 |
| Issue date: | 04/01/1986 |
| From: | ANEFCO, INC. |
| To: | |
| Shared Package | |
| ML20212N417 | List: |
| References | |
| NUDOCS 8608280221 | |
| Download: ML20212N423 (186) | |
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O SAFETY ANALYSIS REPORT CASE AP-101 REVISION 2 APRIL 1, 1986 O
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SAFETY ANALYSIS REPORT CASK AP-101 REVISION 2 APRIL 1, 1986 1
O ANEFCO, INC.
i TABLE OF CONTENTS Chapter 0.0. - General Information 0.1 Introduction 0.2 Package Description 0.2.1 Packaging 0.2.1.1 Shape 0.2.1.2 Size 0.2.1.3 Weight 0.2.1.4 General Construction 0.2.1.5 Primary Containment Vessel 0.2.1.6 Capacity l
0.2.1.7 Shipping Configuration 0.2.1.8.4 Outer Shell 0.2.1.8.5 Closure Ring 0.2.1.8.5 Lid Closure Seal 0.2.1.8.7 Cask ' Bottom 0.2.1.8.8 Cavity Drains, Venting. Drain Seals and Pressure Relief Devices 0.2.1.8.8.1 Cavity Drains i
4 0.2.1.8.8.2 Cavity Venting 0.2.1.8.8.3 Drain Seals 0.2.1.8.8.4 Cavity Pressure Relief Device I
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0.2.1.9 Closure Lid 2
0.2.1.9.1 Tamper P' roof Seal 0.2.1.10.1 Lifting Trunnions 0.2.1.10.2 Rotation Trunnions 0.2.1.11 Impact Limiters 0.2.1.12 Cask Fire Shield 0.2.2 Operational Features 0.2.3 Contents of Packaging 0.2.3.1 Description of Contents 0.2.3.2 Waste Material Canisters
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0.2.3.3 RH-TRU Canisters 0.2.3.3.1 Canister Dimensions O
0.2.3.3.2 Canister Shape y
0.2.3.3.3 Canister Weight 0.2.3.3.4 Canister Materials 0.2.3.3.5 Canister Integrity
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O T-2 Rev. 2 - 4/1/86 J
I Chapter 1.0 - Structural Evaluation
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1.1 Structural Design 1.1.1 Structural Design 1.1.2 Design Criteria 1.1.3 Canister Design Criteria - RH-TRU l.1.3.1 Weight & Dimensions 1.1.3.2 Waste Package Configuration l
1.1.3.3 Materials 1.1.3.4 Structural Integrity j
1.1.3.5 Design Life 1.1.3.6 Internal Pressure & Gas Generation 1.1.3.7 Leak Rate 1.1.3.8 Canister Decontamination O
1.1.3.9 Interfaces 1.2 Weights and Centers of Gravity 1
Table of Cask Weight & Centers of Gravity 1.3 Mechanical Properties of Materials 1.3.1 Table of Mechanical Properties of Materials
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l.4 General Standards for all Packages j
1.4.1 Chemical and Galvanic Reaction I
1.4.2 Positive Closure a
- 1. 4. 3, Lifting Devices 1.4.4 Tiedown Devices f,
1.4.4.1 Lifting Trunnions 1.4.4.2 Rotation Trunnions 1
1.4.4.3 Impact Limiter Attachment i
T-3 Rev. 2 - 4/1/86 t
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2 l 1. 5 Standards for Type B (0) Packaging 1.5.1 Loading Resistance I
1.5.2 External Pressure 1.6.1 Heat 1.6.1.1 Summary of Pressure and Temperature 1.6.1.2 Differential Thermal Expansion 1.6.1.3 Stress calculations 1.6.1.4 Comparison with Allowable Stresses GV T-3a Rev. 2 - 4/1/86 s
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1.6.2 Cold 1.6.2.1 Cold - An Ambient Temperature
-40'F in Still Air and Shade 1.6.2.2 Contraction of Lead Around Inner Shell 7
f 1.6.3 Pressure 1.6.4 Vibration j
1.6.5 Water Spray l
1.6.6 Free Drop ii 1.6.6.1 One Foot End Drop t
1.6.6.2 One Foot Side Drop 1.6.7 Corner Drop i
1.6.8 Penetratior.
I d) 1.7.0 Hypothetical Accident Conditions l.7.1 Free Drop j
1.7.1.1 End Drop 1.7.1.1.1 Impcct Limiters 1.7.1.1.2 End Drop - Components i
1.7.1.2 Side Drop 1.7.1.2.1 Impact Limiters
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1.7.1.2.2 Side Drop - Components 1.7.1.3 Corner Drop, Top & Bottom 1.7.1.3.2 Components (Cover Drop)
I 1
1.7.1.4 Oblique Drop 1.7.1.4.1 Impact Limiters j
1.7.1.4 2 Components (Oblique Drop)
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T-4 ANEPCO. INC.
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1.7.2 Puncture l
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1.7.2.1 Top Puncture j
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1.7.3 Thermal i
1.7.3.1 Summary of Pressures and Temperatures
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1.7.3.3 Stress Calculations 1.7.3.4 Comparison with Allowable t
Stresses I
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Appendix 1.10-1 Cask Mass Moraent of. Inertia Appendix 1.10-2 Energy Transfer O
O T-6 AN EFCO, INC.
I Chapter 2.0 - Thermal Evaluation
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,gg iV 2.1 Discussion 2.2 Summary of Thermal Properties of Materials f
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2.3 Technical Specifications of Components
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l 2.3.1 Figure of Heat Resistance of VITON 2.4 Thermal Evaluation for Normal Conditions of Transport t
1 2.4.1 Analytical Thermal Model t
1 2.4.2 Maximum Temperatures I
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2.4.3 Minimum Temperatures 1
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2.4.4 Maximum Internal Pressure i
I 2.4.5 Maximum Thermal Stresses i
J 2.4.6 Evaluation of Package Performance for i
j Normal Conditions of Transport O
2.4.7 Thermal Evaluation of RH-TRU Canister 2.4.7.1 Package Conditions and Environment j
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e 2.4.7.2 Package: Temperature 1
j 2.4.7.3 Evaluation Summary t
2.5 Hypothetical Thermal Accident Evaluation i
1 2.5.1 Analytical Thermal Model 7
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2.5.2 Package Conditions and Environment f
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,t 2.5.3 Package Temperatures f
2.5.4 Maximum Internal Pressure i
i 2.5.5 Maximum Thermal Stresses i
i 2.5.6 Evaluation I
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2.6 Appendix
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2.6.1 Equivalent Conductivity of Air j
1-Gap 4
i 2.6.2 Description of THERMOS l
i 2.6.3 Calculation of Steady State Surface i
Heat Transfer Coefficients j
2.6.4 Calculation of Transient Surface j
Heat Transfer Coefficients l
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Chapter 3.0 - Containment i
n 3.1 Containment Boundary 1
3.1.1 Containment Vessel 1
3.1.2 Containment Penetrations 3.1.3 Seals and Welds 3.1.4 Closures i
3.2 Requirements for Normal Conditions of Transport I
3.2.1 Release of Radioactive Material j
i 3.2.2 Pressurization of Containment Vessel N
3.3 Containment Requirements for the Hypothetical l
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Accident Conditions 3.3.1 Fission Gas Products 3.3.2 Release of Radioactive Material I
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(Contents)
I 3.4 Containment of RH-TRU 2aste r
3.4.1 Primary Vessel l
3.4.2 Secondary Vessel j
t 3.4.3 Pressurization of Containment i
2-3.4.4 Gas Generation in RH-TRU Waste f
t 3.4.5 Evaluation Summary i
j 3.5 AP-101 Cask Considerations For RH-TRU Waste l
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3.5.1 Hypothetical Release Considerations
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t 3.5.2 Cask Dunnage i
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1 Chapter 4.0 - Shielding Evaluation 4.1 Shielding Evaluation 4.2 Gamma Flux l
4.3 Side Drop Gamma Shielding 1
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i DRAWING INDEX
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Drawing Number:
Title of Drawing Date of Drawing i
i SC 101 Cask Assembly 6/7/76
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SC 102 Assembled Dims. &
6/7/76 f
Weld Details 1
l SC 103 Closure Assembly 6/7/76
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& Details
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SC 104 Lifting & Rotating 6/7/76
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Trunnions i
SC 108 Cavity Drain Ass'y 6/7/76 l
Dets& (10) (21)
SC 110 Impact Limiter Details 6/7/76 l
lih' SC 112 Transport Configuration 6/7/76 j
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0.0 GENERAL INFORMATION 0.1 Introduction i
Al This report presents a safety analysis of the ANEFCO Type B ()
Shipping Cask Model AP-101.
The cask is capable of carrying a gross load of 10,000 pounds of dry, solid, non-fissile metallic waste material.
Typical loads would consist of control rods, velocity limiters, poison curtains, fuel channels, fuel and control rod storage racks, consumable poison rods and similar material, It will also carry the waste form of defense RH-TRU (Remote Handled Transuranic) waste.
The maximum inter-
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nally generated heat load is 0.3kw and up to 1kw during the transport of RH-TRU, The waste form (RH-TRU) will be contained j
in carbon steel canisters.
The cask is designed to meet 10CFR71 related to the shipment of large quantities of radio-active materials.
The principal means of transportation will be by a speciallly designed motor vehicle transport trailer under sole use assignment although all and other modes may be utilized.
The AP-101 Shipping Cask has been designed to provide maximum safety for the shipment of the radioactive material.
Since liquid coolants are not required to remove the internal heat
/~T loads, the problems of contaminated liquid coolant release
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as a result of the hypothetical accident conditions are elim-inated.
Decay heat is transferred from the waste materials to the environmnet first by thermal radiation and convection to the cavity surface and then through the cask sides and ends by conduction, and then by natural convection and radiation from the surface of the cask of the environment.
Being entirely passive, this means of heat dissipation is highly reliable.
0-1 Rev. 2 - 4/1/86 p.
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0.1 Introduction (continued)
Cask weight and typical loads are limited to PT permit legal weight truck shipment (73,280 #GVW) k/
of the cask.
When the cask is loaded to its maximum capacity of 10,000 pounds the cask and maximum load will be less than the legal weight truck shipment of 80,000 #GVW which is standard in 24 states as of January 1,1976.
To-obtain this objective it was necessary to consider the shipping cask and trailer as a system under sole use assignment which primary consideration being given to the shipping cask integrity and relia-bility.
The trai-ler is specially designed to accomodate the cask.
For the purpose of package evaluation the shipping cask with impact struc-tures attached to each end is to be considered as the configuration of the package as present'ed l
for shipment.
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w lbs.
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5 Closure Assembly 2053 206.7 4.24 x 10 446 212.8
.95 x 10 14 Closure Ring 5
8 Inner Shell 3200 118.I 3.78 x 10 3
Outer Shell 10,000 115.3 11.53 x 10 5
25 Inner Shell - Bottom 370 32.5
.12 x 10 Plate 5
24 Bottom Shield Support-240 26.5
.06 x 10 5
21 Bottom Plate 1200 22.75
.27 x 10 Lifting Trunnions 1052 188.
1.98 x 10 5
Rotating Trunnions 490 46.
.23 x 10 4
Gama Shield 27,066 116.3 31.48 x 10 5
6 Bottom Lead Shield 757 30.0
.23 x 10 5
1 Thermal Shield 1255 116.
1.46 x 10 5
I 42 Impact Limiters Assemblies 3446_
118.
4.07 x 10 l
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60.40 x 10 Ewy I
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5 Contents 10,000 116.3.
11.63 x 10 f
61,575 Loaded W EW3 3
5 72.03 x 10 EFw 117' Loaded C.G.
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- For Identification of Part Nos., see ANEFCO Drawings SC101.
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0.2.1.4 General Construction The materials of construction are: stain-less steel (used in the structural members as well as threaded fasteners), cask chemi-cal grade lead (used for gamma shielding),
plate aluminum, balsa wood hernetically sealed in an aluminum alloy canning ( sed in the impact limiters), and high tempera-ture clastoner seals.
The primary containment structure of the AP-101 Cask is fabricated free ASTM A?d0, Type 3-4 stainless steel.
The inner and outer shells of the cask body are both welded to the closure r.ing at the top of the cavity flange.
Both shells are welded at the bottom to their.own separate bottom closure plates.
The annulus between the outer and inner shell is filled with lead for g'amma shielding.
She botton closure plate of the 1.5 inch thick outer shell consists of a 3 1/2 inch stainless steel plate.
A 4 inch thick, 29 3/4 inch diameter aluminum plate is mounted to and
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centered on the 3 1/2 inch thick bottom plate to create a controlled void volume in the cask lead gamma shielding at the bottom of the cask Belted on impact limiters at each end of the cask serve as energy absorbers for the hypothetical accident drops.
These two energy absorbing structures are formed of balsa wood totally enclosed within hermetic aluminum alloy canning.
Four cask lifting trunnions (redundant pairs for those sites requiring four-point lifts) are attached to the upper outer shell of the cask, and two cask rotating trunnions are attached to the lower shell of the cask.
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ss The bolted on cask lid consists of an outer stainless steel plate which is fastened to the closure ring and an inner stainless steel weldment which contains the lead shielding for the upper end of the cavity.
0.2.1.5 Primary Containment Vessel The containment vessel is the 5/8 inch thick inner cavity shell and 2 1/16 inch thick bottom closure plate.
The con-tainment vessel, including all penetrations is fabricated of 304 stainless steel.
The cask cavity is closed and sealed by a bolt-on-plug-type closure lid consisting of a 2 inch to 3.5 inch thick outer p1' ate and a steel weldment containing lead shielding which extends into the cavity opening.
Plug seals for the two cavity drains are located in the drain connection fittings which are welded to the cavity bottom closure plate.
0.2.1.6 Capacity The AP-101 Cask is capable of accommodating a grcss load of up to 10,000 pounds of solid, dry, metallic, non-fissile materials, such as, but not limited to, control rods, poison curtains, fuel channels, and fuel storage racks.
0.2.1.7 Shipping configuration Transportaticn of the AP-101 Cask is nor-mally by (sithough not limited to) truck shipment with the cask in a horizontal position, carried on a specially built transporter.
The transporter is basically of reinforced beam type construction.
A protective personnel barrier cover shield l
is not required.
Two of the four lifting trunnions are used as cask tie-downs to support the entire load of the cask and its contents under the 10g axial load conditions.
The transverse and vertical imposed loads of normal transport are shared between three i
of the lifting trunnions and the two rota-ting trunnions.
The clamps for the rotating trunnions allow for expansion and contraction f-()
differences between the cask and the trans-porter.
0-6 ANEFCO, INC.
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! rs (N"3 0.2.1.8~.4 Outer Shell l
V The outer shell is a 39.25 inch outside diameter, 1.5 inch thick.stcinless steel cylinder.
The shell is welded to the
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closure ring and a 3.5 inch thick stain-(
less steel bottom plate.
Two cavity drain holes located 120 degrees apart are the only penetration of the outer shell.
0.2.1.8.5 Closure Ring The closure ring is a stainless steel ring, l
39.25 inch O.D.,
28 inch I.D.,
and 3.5 inches thick.
The ring is welded to the inner and outer shells to form the top closure for the' lead shield cavity.
Twenty 1-1/2 inch diameter holes with helically coiled thread inserts are provided for bolting the closure lid to the ring.
Two 1.75 inch diameter guide pins located 172 degrees apart are threaded into the ring to assist with align-ment of the lid during closure operations.
0.2.1.8.6 Lid Closure Seal
- '()
The seal between the closure lid and ring is made of high temperature, concentric rings of an elastomer material which are bonded to both sides of a flat retainer of stainless steel.
The seal assembly called a "Gask-O-Seal" by the manufacturer is fastened to the underside of the cask lid and seals against the flat machined surfaces of the cask lid and the closure ring.
The lid is bolted to the closure. ring by twenty, 1 1/2 inch l
diameter hex bolts: Bolt heads bear on the cask lid, the shanks penetrate through the lid flange and thread into the closure ring.
0.2.1.8.7 Cask Bottom The cask botton consists of a stainless-1 steel disc with a 39.25 inch 0.D., and 2
a 3.5 inch thickness.
The disc is welded to the outer shell to form the bottom closure for the lead shield.
,.O 6-7 ANEFCO, INC.
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0.2.1.8.8 CAVITY DRAINS, VENTING, DRAIN SEALS AND PRESSURE RELIEF DEVICES i
0.2.1.8.8.1 Cavity Drains r
The cavity is drained through two 1.5 inch, O.156 wall pipe connections between the bottom of the cavity and the lower end of the outer shell.
These drains also pass through the lead shielding.-
0.2.1.8.8.2 Cavity Venting Venting of the cavity for draining is accomplished by air supplied at the maximum pressure of 5 psig through one of the two Cavity Drain Connections.
0.2.1.8.8.3 Drain Seals Each of the two cavity drain lines are sealed with two radial "O" ring seals mounted on a plug which is threaded into the drain opening in the inner elbow which is directly welded to the cavity bottom
.(3 plate.
The "O" rings are seated against
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the I.D. of the drain line opening.
A weather-tight cover seal plate is provided for each drain access opening.
0.2.1.8.8.4 Cavity Pressure Relief Device No Pressure Relief Device is used in the AP-101 Cask as the cask is specifically intended for the shipment of dry, solid, metallic, non-fissile non-volatile loads. The i
maximum internal pressure under the hypo-i thetical accident is less than 20% of the design pressure.
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0-8 ANEFCO, INC.
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- 0. 2.1.9 CLOSURE LID Ov t
0.2.1.9 Closure Lid y
The lid is bolted to the 39.25 inch diameter closure ring; is fabricated from 3.5 inch thick stainless steel plate and is welded to a stainless steel structure which contains the top lead shield.
The plug portion of the lid has a radial clearance less than that of the lid bolts clearance holes, preventing contact of the lid with the closure bolts during the hypothetical accident conditions which would put a shear load on the closure bolts.
There are twenty counterbored clearance holes for the 11 inch closure bolts and two 1 inch holes for the lid l,ocating guide pins.
The top surface of the lid.has four one inch diameter, helicoil inserts in blind-threaded holes for attachina the lid liftinc bolts.
A seal test connection is provided in the lid.
l the seal test connection is in turn sealed by redundant radial "O" ring seals mounted on a closure plug which is threaded into the lid and recessed below the top surface to prevent accidental damage to the plug.
f
'O.2.1.9.1 Tamper Proof Seal j
()
The cask is provided with security wire seal blocks that provide means for detecting tampering with the
'i loaded cask after a wire seal is placed in position.
2 One seal block is welded to the cask lid and a second seal block is welded to the cask body.
Each meal block l
is inch tall by inch thick and has a 3/32 inch hole through which a wire is pulled and sealed to verify l
that no tampering has occurred with the cask. (See SK-108) 1 0.2.1.10 Lifting Trunnions l
Four 8 inch diameter by 3 inch long flanged trunnions are located 90 apart on the upper part of the outer shell of the cask body.
Each pair of opposite lifting
]
trunions is designed in accordance with the regulations and may be used independently of each other.
The four trunnion design-is used to meet the requirements-of those reactor sites which require independent four point lifts for insertion and removal of the cask in the reactor's storage pools.
The lifting trunnions are located just I
below the upper impact limiter and are protected against contact with the unyielding surface in the side-drop test by the upper impact limiter.
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- 0.2.1.10.2 Rotation Trunnions '- '
Located on either side of the lower part,,
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of the outer shell are two 8 inch diameter by 3 inch long trunnions for totating the cask to and from the horizontal position are offset from the cask centerline so that when the cask is lowered onto the trailer, it will rotate in a preferre.d direction to the horizontal position as the crane hook is lowered.
The rotating impact limiter are protected against con-tact in the side drop accident by the lower impact limiter.
O.2.1.11 Dr. pact Limiters Removable impact 1Lmiters are located at each end of the cask body to absorb the energy of a drop accident.
Each impact limiter is constructed of pretreated balsa wood blocks enclosed within an aluminum structure which is bolted on to the ends of the cask body.- These two impact limiters are removed from
(< s_)
and attached to the cask body while the cask is in the horizontal position on the transport trailer.
The impact limiters may be stored on the transport trailer whenever the cask is removed from the trailer.
0.2.1.12 Cask Fire Shield The outer shell is thermally insulated against the heat from the hypothetical fire by a stand-off hermetic airgap cover constructed of 0.135 inch thick stainless steel sheet.
This fire shield has a 2B finish on the exterior surface as an aid in decontamination of the cask after removal from the pool.
The impact limiters provide.
thermal insulation for each end"of the cask.
9 O
0-10 AN EFCO, INC.
()
0.2.2 Operational Features The ANEFCO AP-101, i'ype B Large Quantity Cask is not a complex package system as it is not used for fissile material and hence does not require a neutron shield nor fluid cooling means to dissipate the small (150 watts) internal thermal loads of the contents to be shipped in the cask.
0.2.3 Contents of Packaging 0.2.3.1 Descriotion of contents l
i Contents to be transported in this cask will be i
of the non-fuel bearing type; control rods, fuel channels, activated components and filter elements.
All materials will be packaged in disposabl&
inner containers.
The waste form of defense RH-TRU waste will also be transported in this cask.
The RH-TRU waste will be contained in carbon steel canisters.
The wastesform nuclides and average qualitative description is shown in Chart A.
The waste as
()
described is defined as transuranic waste (RH-TRU, remoate handled transuranic waste) and is character-!
ized by those radionuclides which are so indicated.
The principal activities (nuclides) are indicated on the chart.
Samples of D.O.E. waste were analyzed at the major facilities to establish the norm.
The A2 factor for the worst case hypothetical accident and the WIPP waste acceptance criteria (WIPP-WAC) were used to postulate release rates.
Reference Section 3.4.2.
2 Those isotopes which could be potentially present in a canister are defined as follows:
TRU:
Am-241, Cf-249, CF-250, Cf-252 i
Cm-243, Cm-245, Cm-246 Pu-239, Pu-240, Pu-242 U-233 Non-TRU:
mixed fission products f~
Sr-90, Ac-227, Pa-233 k}/
0-11 Rev. 2 - 4/1/86 I
I CHART A g
TYPICAL ISOTOPIC COMPOSITION & CONTAINED ACTIVITY IN 55-GALLON DRUM
- Gross Weight:
50 kg MASS (g)
ACTIVITY (Ci)
NUCLIDE Ag (Ci)
Am 241 0.008 2.7 E-4 9.1 E-4 Cf 249 0.002 3.9 E-10 1.6 E-9 Cf 250 0.007 3.8 E-10 4.2 E-8 l
Cf 252 0.009 3.9 E-9 2.1 E-6
)I Cm 243 0.009 2.2 E-6 9.9 E-5 Cm 245 0.006 3.9 E-5 6.8 E-6
(])
Cm 246 0.006 2.7 E-3 8.3 E-4 Pu 238 0.003 3.8 E-5 6.6 E-4 Pu 239 0.002 2.3 E-2 1.4 E-3 Pu 240 0.002 5.6 E-3 1.3 E-3 Pu 242 0.003 8.4 E-5 3.0 E-7 U
233 0.03 2.0 E-7 1.9 E-9 TRU Waste Concentration: 140spCi/kg J.E. Bigelow to T. Grizzard - ORNL Intra Lab Memo Dated October 23, 1984.
0-lla Rev 2-4 /l'/ 8 6
+
(%
%)
O.2.3.2 Waste Material Cannisters The solid waste material will be preloaded into disposable metal cannisters similar to that shown in Figure 0.2.1.9 for insertion to shipping cask.
l 0.2.3.3 RH-TRU Waste Cannisters 0.2.3.3.1 Canister Dimensions The engineering drawings of the typical canisters proposed for the shipment of RH-TRU waste are shown~in Figures H-2-91273-1 and H-2-91273-2.
Typical drawings show that the canisters will be fabricated of carbon steel.
Canisters will be 26 inches outside diameter and 10'l long.
The canister will be braced by dunage to prevent dynamic motion within-the cavity as shown in Figure SZ-5.
[
2 0.2.3.3.,2 Canister Shape The shape of the canister will_be a right angle j
y,
()
cylinder.
O.2.3.3.3 Canister Weight The empty canister will weigh less than 1000 lbs.
i and filled canisters will weigh less than 10,000 lbs. when filled.with RH-TRU waste.
0.2.3.3.4 Canister Materials r
The materials of construction will be carhon steel.
0.2.3.3.5 Canister Integrity The canister structural integrity will be suffi-cient to withstand toutine operations, conditions for Type A shipment (reference 49CFR173.398).
P 0-llb Rev. 2 - 4/1/86 (V
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1.0 STRUCTURAL EVALUATION f7,
<()
1.1 Structural Design The principal structural members of the package can be separated into two major structural sys-tems and other components.
The primary contain-ment is made up of the inner shell and its bottom plate, the closure ring and seals, the closure bolts and closure assembly.
These components are designed to contain the contents under maximum conditions of cavity pressure and temperature and prevent puncture from the top.
The next major structural system is the shielding envelope which is composed of the closure ring, outer shell and bottom plate.
These components keep the lead shield intact and prevent puncture from the side and bottom.
The third protective system is made of the energy absorbers which are bolted on each end.
Penetration of the primary containment occurs at the two bottom drains which are protected by a threaded insert and machined housing.
Access to the drain plug is through a tube designed to with-stand normal operating conditions.
This tube may also withstand the hypothetical accident condi-gm
(_)
tions, but even if it does not, the primary con-tainment will not be violated even if this tube fails.
Lifting and rotation trunnions are also provided that are used for operation and tie down.
During shipment of RH-TRU waste, the cask will serve as the outer protection for the shipment.
However, the 2
canisters will serve as the primary containment to contain the contents and to withstand routine operations and conditions for Type A shipments in conformance with 49CFR173.398.
1.1.2 Design Criteria The design conditions used to evaluate the struc-tural integrity of the packaging and specified in 10CFR71.
Specific paragraphs that apply are 71.31, 71.32, 71.35, 71.36, Appendix A; Condition 1 to 6 and 8, Appendix B; Conditions 1 to 3.
1-1 Rev. 2 - 4/1/86
o
[
Y
- 1. 'l. 2 Design Criteria (continued)
()
g#
For the primary containment vesiel, design-con-j ditions of 600'F and 100 psig. were used with the assumption that it is a free standing vessel with no support from the lead.
All cask com-ponents and structures were designed to with-stand an acceleration of 50 g's in any direction.
The theory of failure used for this SAR, was the maximum shear stress theory.
In general, the approach in the ASME Boiler and' Pressure JlVesselCodeSectionIIIwereusedtosizecom-ponents, obtain material properties, and evaluate design safety margins.
Both operating and accident conditions were evaluated and compared J[with the stress and fatigue limits in Section III.
When specific design formulae were available, such as presented in ORNL-68, these were used to either size or evaluate components and parts.
Design criteria used to evaluate stresses and strains caused by the 30 foot Free Drop and the 6 inch bar puncture were either the static yield, or where appropriate by comparison with the dynamic yield or ultimate tensile strength.
w Permanent deformations were allowed to occur provided that the ultimate strain was not reached and the primary containment seals remained operable.
I i
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s 1-2 Rev 2 - 4/1/86 1,
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i l.1.3 CANISTER DESIGN CRITERIA i
i 1.1.3.1 Weight and Dimensions The typical canister diameter shall be nominally 26 inches (0.66m) and shall not exceed 121 inches (3.07m) in length including the pintle.
The canister 6
weight dNdl be the minimum achievable while meeting other applicable criteria.
1.1.3.2 Waste Package Configuration All RH-TRU waste package external surface shall be.a smooth-sided cylinder and shall not have protrusions beyond the nominal outside diameter of the canister.
{
The handling appurtenance dull be a pintle, shown in I
Figure 1, welded at the top centerline of the package.
1.1.3.3 Materials
}
The canister body, end caps and pintle shall be fabri-i cated from carbon steel.
The external surfaces shall Q'1 be coated with acryllic enamel or other anti-corrosion coating.
If material other than carbon steel are used for sealing, filtered vents, etc., they shall be compatible with carbon steel.
1.1.3.4 Structural Integrity 4
The canister structural integrity shall be sufficient to withstand routine operating conditions, conditions for Type A packaging and retrieval after storage. The environmental and test conditions for Type A packaging
(
are as follows:
1.1. 3. 4.1 Standards for Type A packaging:
f 1.
Type A packaging must be so designed and constructed that, if it were subject to the environmental and test conditions prescribed in this paragraph; (1) There would be no release of radioactive material from the package; (11) The effectiveness of the packaging would not be substantially reduced; and (111) There would be no mixture of gases or vapors in the package which could, through any credible increase of pressure or an explosion, significantly reduce the m
effectiveness of the package.
1-2a Rev. 2 - 4/1/86
i
/'b
{
1.1.3.4.1 cont.
2.
Environmental conditions:
1 (1) Heat. Direct sunlight at an ambient temperature i
of 130'F in still air.
(11) Cold, an ambient temperature of -40*F in still air and shade.
l (111) Not Applicable (lV) Vibration. Vibration normally incident to trans-portation.
3.
Test conditions:
The packaging shall be subject to all of the following tests unless specifically exempted there-from, and also to the consecutive application of at least two of the following tests from which it is not specifically exempted:
(1) Not Applicable (11) Free drop.
A free drop through a distance of 4 feet onto a flat essentially unyielding horizontal surface striking the surface in a
' position for which r.aximum damage is expected.
(-)
(_/
1 (111) Not Applicable (lV) Penetration.
Impact of the hemisphereical end of a vertical steel cylinder ik inches in diameter and weighing 13 pounds dropped from a height of 40 inches onto the exposed surface of the package which is expected to be most vulnerable to puncture.
The long
[
axis of the cylinder shall be perpendicular to the package surface.
(V) Not Applicable 1.1.3.5 Design Life The RH-TRU waste canisters including labeling shall have a design life of 25 years.
1.1.3.6 Internal Pressure & Gas Generation The canister shall have provisions for continuous venting of gases through a HEPA type filter under normal conditions.
1.1.3.7 Leak Rate
()
The gas pressure drop leakage test or equivalent shall be used to demonstrate the final closure seals effective-ness of the RH-TRU waste canister.
The filter shall be closed during this test.
The test shall be conducted l
l-2b Rev 2 - 4/1/86
(
O in accordance with requirements in ANSI N14.5, "American National Standards for Leakage Tests on Packages for Shipment of Radioactive Materials".
1.1.3.8 Canister Decontamination The'outside of the canister shall be designed to facilitate surface decontamination and cleaning.
i 1.1.3.9 Interfaces l
l Coordination with the following interfaces shall be i
maintained to assure that the waste canister design and the interfaces are compatible:
(1) empty and full canister handling and storage system, (2) filling equipment and procedures, (3) sealing and inspection equipment, (4) handling and transporting systems, and (5)the handling, transporting, emplacement and retrieval systems.
()
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(
1-2c Rev 2 - 4/1/86
N O
1.2 Weights and Centers of Gravity The individual weights of the major individual sub-assemblies are tabulated in the. table of Cask Weight and Centers of Gravity.
Each sub-assembly is referenced to the Cask Assembly, Drawing #SC-101, respectively.
The total empty cask weight is 51,575 pounds and the weight of the cask with the maximum design load is 61,575 pounds.
l The center of gravity of the loaded cask is 117 inches above the bottom of the cask assembly with the outer edge of the impact limiters as the reference point.
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x Table of Cask Weight & Centers of Gravity
- Pdrt {
w lbs.
E in s' wY C.G.
5 Closure Assembly 2053 206.7 4.24 x 10 5
14 Closure Ring 446 212.5
.95 x 10 8
Inner Shell 3200 118.1 3.78 x 10 3
Outer Shell 10,000 115.3 11.53 x 10 25 Inner Shell - Bottom 5
Plate 370 32.$
.12 x 10 5
24 Bottom Shield Support-240 26.$
.06 x 10 5
21 Lottom Plate 1200 22.75
.27 x 10 Lifting Trunnions 1052 188.
1.98 x 10 5
Rotating Trunnions 490 46.
.23 x 10 5
4 Gamma Shield 27,066 116.5 31.48 x 10 5
6 Bottom Lead Shield 757 30.0
.23 x 10 5
1 Thermal Shield 1255 116.
1.46 x 10 l
42 Impact Limiters Assemblies 3446 118.
4.07 x 10 W
=Ew 51,575 T
5 60.40 x 10 Ewy 117" CG = l [_w E*'
l 5
Contents 10,000 116.3.
11.63 x 10 e
61,575 Loaded W EW3 3
5 EFw 72.03 x 10 117" Loaded C.G.
O
- For Identification of Part Nos., see ANEFC0 Drawings SC101.
1-4 1
ANEFCO, INC. '
}
1.3 MECEANICAL PROPERTIES OF MATERIALS The following materials will be used in the fabrication of the cask.
The mechanical properties are listed in Table Nol.3-1 on the next page.
- 2. All structural members, drains, fire shield and accessories:
ASTM A240, Type 304 for plate, ASTM A213, Type 304 for tubo and ASTM A312, Type 304 for setmicss pipe.
- 3. Closure Bolts, Lifting and Impact Limiter Attachment Bolts: ASTl! A320, Grade L43.
- 4. Impact Limiter' Outer Shell:
Aluminum Alloy 6061-T6.
3 { 5. Balsa Wood
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O l-5 Rev 2 - 4/1/86 ANEFCO, INC.
2Qr TABLE 1.3.1 MECHANICAL PROPERTIES OF MATERIALS
'a I
Spec.
Spec.
Min.
Min.
MATERIAL TEMPERATURE Material Yield Tensile 100 300 400 500 600 REFERENCE SA-240, Type 304 30.0 75.0 SM 20.0 19.8 17.6 16.4 15.6 SA-213, Type 304 SY 30.0 22.5 20.7 19.4 18.2 SA-312, Type 304 MEAN 9.16 9.47 9.56 9.70 9.82 E
29.1 28.3 27.7 27.0 26.0 SA-320, Grade L43 105.0 125.0 35.0 31.9 30.6 29.5 28.1 E Lead Yield Strength -860 psi; Dynamic Strength - 5000 psi.
(1) (2) (3)
~
Balsa (11 lb/ftf Compressive Strength - 1910 psi.
(4)
Aluminum Alloy 6061-T6 UTS = 45,000 psi; MTS = 40,000 psi; USS = 27,000 psi.
E = 10.0 x 106 psi;
= 0.33 N<
" (1)" Nuclear Engineering and Design", Vol. 13,1970, North-Holland Publishing Co., P.O. Box 3489,,
8 Amsterdam, The Netherlands.
e L.,
" Cask Designers Guide," ORNL-NSIC-68, United States Atomic Energy C - insion,h '.;i' 2 (2) Shappert, Oak Ridge, Tennessee.
4 g (3) Goldsmith, W., " Impact-The Theory and Physical Behavior of Cooliding Solids," Edward Arnold:QJ Publishers, LTD. 1960.
1,',,
m (4) Ref.1:
'E I
Balsa Ecuador Lumber Corporation Data Sheet No. 70, 1963.
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_mi__________-..__,.---_.--_-m___._
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-nL) 1.4 General Standards for all Packages t
t t
l 1.4.1 Chemical and Galvanic Reaction
.+
b The cask's materials of construction, those of the disposable canister and the contents are all metals that do not produce signi-ficant chemical galvanic or other reactions.
The packaging components are either stainless steel, lead or carbon steel.
The contents are carried in a. disposable carbon steel I
i canister which is carried in the stainless I
steel primary containment.
These...;erials do not have any significant adverse inter-t 1
actions.
l i
1.4.2 Positive Closure L
The closure system is made of positive screw t
- /~}
type devices that must be deliberately opened i
'k and cannot be accidentally activated.
The closure assembly is secured by 20 bolts 1-1/2 inch in diameter, each of the two drains are closed by a one inch externally threaded screwed i
plug (allen head or hex head).
This drain is i
then closed at the outer shell by a 1-1/4 inch externally threaded cap plug.
Therefore, the closure bolts and drain plugs cannot be inad-vertently. opene.d.
?
1.4.3 Lifting Devices The following two sections show that the lifting devices do not yield under three times the operating load, The subsequent sections show that failure would~not impair containment or I
shielding.
j t
t l-7 ANEFCO, INC.
O
. y,V Trunnions The cask has two sets of trunnions; lifting trunnions and rotation trunnions.
The four lifting trunnions are located near the upper (closure) end of the cask, and the rotation trunnions are located at the lower (base) end of the cask.
Any of the lifting and i
rotating trunnions will withstand the trans-port loading conditions without exceeding the yield strength of the component material.
The transport acceleration load produces a maximum trunnion force of 3.5 W in each of the three lifting trunnions used for tiedown, i
which is more than the trunnion force produced by the design lifting load of three times the cask weight.
This static design load produces a force of only 1.5W in each trunnion when only two lifting trunnions are'used.
(See section 1.44 for the analysis of Tie-Down Devices).
I Closure Lifting Bolts hb/4 J's N
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V Figure 3W Closure Assembly Lifting Device O
1-8 ANEFCO, INC.
r 17' 4
7)
The closure assembly lifting device is attached
(,
to the lid by four 1 inch diameter 12UNF bolts.
The vertical force on each bolt (considering three times the 2,500 lb. weight of the cask lid) is:
(3/4) (2,500) = 1875 lbs.
F
=
y The direct tensile stress in the bolts is:
~
(F /A )= (1875/0.662) = 2,832 psi.
T=
B The shear stress through the root area has a maximum value of:
l'= F /A h
B based on the lifting spider geometry.
where Fg=Fy T =
(T. = 2,832 psi.
The effective stress intensity is:
~
1/2 Sg=2
((T/2)2 + 4:2 0
S
= 6,300 psid s (105,000 psi) i Y
The internal threads in the lid do not have to be checked because the helically coiled inserts are at least one bolt diameter long (ref. Marks)
^
Failure of Lifting Devices Under Excessive Load Would Not Impair the Containment of Shielding Failure of the cask lifting devices would not harm the primary containment or shielding.
Loading conditions beyond the design load would cause the trunnion to fail in the trun-nion tubes at the interface between the trunnion tube and mounting plate.
This is true for both the lifting and rotation trunnion as shown in section 1.4.4.
This type of failure would not cause a puncture of the outer shell, loss of a seal or failure of the inner shell.
r~%
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1-9 ANEFCO, INC.
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Failure of the lid lifting bolts by excessive loads also would not affect the cask integrity or shielding.
I 1.4.4 Tiedown Devices No Yielding with 10-g Longitudinal, 2-g Vertical, 5-g Transverse Force Combined Tiedown Loading The anchorage point of the cask to the trans-port vehicle are at the lifting and rotation trunnion.
There.are a total of five tiedown points; three lifting trunnions and two rotation trunnions.
The lifting trunnions will resist all three acceleration components while the rotation trunnions will resist only the vertical and transverse forces.
The resultant force on each of the five trunnion points considering only the 2-g vertical and 5-g transverse forces is equil to 1.08W. Adding this to the 10-g long'itudinal force on the three lifting trunnions increases the lifting trunnion load to 3.5W.
The force of 3.5W acting on the lifting trun-nion is greater than the force produced by the design load for lifting devices, vis. 1.5W (Section 1.4.3).
Thus the loading conditions for t'he lifting trunnions treated as tiedown members is the limiting condition.
Trans-portation forces in the rotation trunnions are less than 1.5W.
1.4.4.1 Lifting Trunnions The lifting trunnions are made from 8 inch schedule 120 stainless steel pipe' (8-5/8)in.
4 O.D.,
0.718 inch wall).
A full penetration weld attaches each trunnion to a 1.125 inch mounting plate.
The plate is in turn welded to gusset plates welded to the main body of the cask. Figure 1.4.4.1 illustrates the lif ting trunnion design.
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ff",A f
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_ ( '&, ' 7.
- ,/,
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4 i
=
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U1
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FIGURE 1,4.4.1.
l LIFTING TRUNNIONS DETAIL J
i 1-11
F n
W f4 Trunnion The moment at the base of the trunnion is:
M
= 1.5 F
= 5.25W T
T where:
W= 60,000 lbs.
The bending stress at the base of the trunnion is:
y = YgB S
y where:
4
= 33.7 in.3 (section modulus) aT (5.25) (60,000)/(33.7) = 9,350 psi.
S
=
b The shear stress at the base of the trunnion is determined by:
8
,, 0 t,- r /a T
T where:
A
= 18.6 in.2 (cross sectional area T
of trunnion)
IT=
(3.5) (60,000)/(18.6) = 11,300 psi,.
The above stresses combine to give an effective stress intensity of:
S=2 (9,350/2)2 + (11,300)2 1/2 S = 24,4 00 psi. <, Sy (30,000)
(
t i
i-O 1-12 ANEFCO, INC.
~
e f
Trunnion Box The bending stress at the base of the box section which attaches to the main body of the cask is:
(9.5) (3.5) (60,000) /EB S
=
B WHERE:
3
= Section modulus of box base 4
(11.75)4 / (12) (6.375)=96.3 in (12.75)
E
=
B 0,700 psi.
S
=
B The shear stress at the base of the box section is:
!^B T
B where:
A
= 12.752 - 11.752 = 24.5 in.2 B
T
= 8,600 psi.
B and the stress intensity is:
S=2h20,700/2)2+ (8,600)2 V2 S = 26,900 psi 4 S (30,000) y Trunnion Mounting Plate The model for the trunnion nounting plate is shown in Figure 1.4.4.3 M T V
/.
/
l J
~
qb-
-a-
.A Figure 1.4.4.3 Lifting Trunnion
'M Mounting Plate ANEFCO, INC.
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Q
,L-g V
The maximum stress in the mounting plate is (1) 2 (cl/4) ('Mt/ah )
S
=
(0.5 ) ' (6 + 6 YT = 7.24 in.
a=
b = 4.3125 in.
(19.54/58.48) = 0.686 l
(Nd2)
=
h = 1.125 in. (plate thickne'ss) l S
= 0.686 (1.5) (3.5) (60,000)/(7.24)(1.125)2 max S
,= 23,600 psi. ( Sy (30,000) l Based on this analysis, the lifting and rotation trunnion j
design is satisfactory.
4
.i l
1 lO I
i I
i 4
I I
(1) Timoshenko. et. al.; " Theory of Plates and i
Shells," Second Edition, Mc Graw Hill,1959.
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1-14 ANEFCO, INC.
i
f
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- v_-
i eQ l.4.4.2 Rotation Trunnions The rotation trunnions are offset 3 inches from the vertical center line of the cask.
The offset position assists initial rota-e tion of the cask toward the horizontal i
shipping position during placement of the cask into the transport vehicle.
During transport the rotation trunnions also serve as tiedown members for the cask but only to restrain the vertical and transverse force The rotating trunnions and the lift trunnions-i' except for the 3 inch offset are identical.
The stress analysis of the rotating trunnions
(
are the same as that for the lifting trunnions as previously described.in Section 1 4.4.1.
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- 3 OFFSET
--. I
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notezion Trunnions oesien ANEPCO, INC.
1-15
'"T 1.4.4.1 Impact Limiter Attachment The impact structures are bolted to the cask body as shown below.
The bolted attachments are designed to secure the impact structure to the cask under the loading imposed by the
' normal conditions of shipment as specified by 10CRF71.31 (d).
Vertical and lateral loads are transmitted directly to the cask j
itself by the cylindrical inner surface of the balsa end caps.
The center of gravity of the caps is within the cask outline, thus, there is no overturning moment.
The 10-g loading in the direction of travel, axial relative to the cask, is taken in tension by 6 bolts 3/4" - 10 parallel to the cask axis.
l l
Weight of Top Impact. Structure = 800 lbs.,
Weight of Bottom Impact Structure = 800 lbs.1 i
l*
Maximum axial force =8,000
-s J
Design axial force =10 Ob i, _ '(L
- 1. __((
L_
' 2h, I AL.ELCCK I
x lbs.
3 Bolt Loading 3/4"-10
.SxlO HFLP 00L Stainless Steel Bolt g
p)4*1 7 lle'Eh!
~]
I'-- - -
Yield Point = 30,000 psi Ten'sion Area = 0.334 in.b
--)
[-
~~
Strength at Y.P. = 10,020 lbs.
y w fy Load on each bolt = 10,000/6 = I 1,700 lbs.
CASK BOI Y S = 5,100 psi (,Sy (30,000) l l
l s
AN EFCO, INC.
()
1-16
[
i 1.
k ft 4
Stainless Steel Lug - Weld Stress Moment on weld at base of lug (base is 1"x2")
(1,700) (1. 75) = 3,000 in. lbs.
(2) (1)/6 =.0.333 in.3
(
b = 3,000/0.333 = 9,000 psi.
S l
S
= 1,700/2 = 850 psi s
1/2 l
S = 2 l"-(3,000/2) 2 + (350)2 l
Aluminum Block, 6061 - T6 Alloy Internal Threads 3/4" - 10 x 1" deep
{
i
= 1.076 in.2 Shear area at Pitch. Dia. = (.5) (3.14) (.685) 1 t
S = 1,700/1.076 = 1,600 psi.<S (27,000)
No credit was taken for the additional shear strength provided by the Helicoil Insert.
- ()
al 1.5 Standards for Type B (U) Packaging 1.5.1 Load Resistance i
Considering the cask as a simple supported, uniformly loaded beam carrying five times its own weight, the maximum bending stress is-l S = SWLC/8I t
where W = 60,000 lbs.
L = 190 in. (distance from the closure to the bottom plate) i C = 19.6 (outer shell outside radius)
I = 31,600 in.4 (outer shell caly) i S = 4,420 (Sy (30,000) psi.
i
()
Rev 2 - 4/1/86 i
1-17 ANEFCO, INC.
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1.5.2 External Pressure To evaluate the effect of an external pressure of 25 psig. the stresses on the outer shells, closure lid and bottom plate are calculated.
The outer shell stress, PR/t is equal to 330 psi which is well below the buckling or membrane stress limit.
Treating the lid and bottom plate as simply supported the stresses are:
S = (6) (0.206) PR /t2= (1.236)(25)(19.6)2/ (3. 3) 2 2
S = 970 psi (1.5 Sm (30,000) 1.6.1 Heat 1.6.1.1 Summary of Pressure and Temperatures The cask is designed to safely contain non-fissile reactor components under all normal operating conditions.
These conditions include the extremes of high and low ambient
/'S temperature, full solar load and full decay kJ heat load.
The only thermal limitation on the cask con-tents is that the maximum internal heat generation should not exceed 0.3 KW.
Under the condition where cask is exposed to direct sunlight in still air at an ambient temperature of 130*F, a maximum internal pressure of 2.6 psig was calculated.
This is well below the 100 psig interr.al design j
pressure of the primary containment.
The corresponding maximum surface temperature of the cask is 180*F.
This is equal to the 180*F maximum accessible surface temperature allcwed by regulations.
During normal operating conditions the cask will go from an isothermal condition.of -40*F to a maximum uniform temperature of 179'F.
O AN EFCO, INC.
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1.6.1.2 Differential Thermal Expansion With a decay heat load of 0.3 KW, at 130*F ambient, with full solar load, the cask is at a uniform temperature of 179'F.
In the radial direction this would produce inter-ference between the outer shell and the lead sheild.
These stresses are less than those produced between the inner shell and the lead shield at the -40*F conditions.
The only problem created by differential thermal expansion problem at the 179'F condition, is the differential axial expansion between the inner and outer shells.
Axial Problems In the axial direction a differential thermal expansion exists between the inner and outer shell because of a possible temperature difference.
From Section 2.4.5, the maximum temperature difference between the inner and outer shell is less than 0.2*F.
Using 0.5'F Os as a design condition, the total difference in thermal expansion is:
6 Z1L =e<L 4T = (9.5 x 16 ) (175) (0.5) = 0.0008 in.
The effect of this amount of differential axial expansion will induce stresses in the drain tube between the inner and outer shellr.
Drain Line Stresses The drain line stresses caused by the differential axial thermal expansion are self-limiting and should be anal zed only as a fatigue problem.
DV l-19 ANEFCO, INC.
~-
< eg Roark, Case 5d, p. 106 1
V (drain in 1-3/8 o.d. tubing,1-1/4 IPS, 1.375 0.D.
O.120 wall) 4-i J
+>
s M6 1
u i
l 6
L n
4 s
RB g
M'= 6 EI 4/L2 V=R
= 12EI d/L3 A
6 at 200*F; E = 27.7 x 10
- pgi, 2
L = 3.5 in. ; A = 0.473 in 4
I = 0.094 in
- C = 0.688 in.
Bending Stress S = MC/I = 6EdC/L2= (G) (27.7 x 10 ) (0.008) (0.688)/12.25 S
= 74,700 psi O
Shear Stress 6
V/A = (12) (27.7 x 10 ) (0.094) (0.008)/(42.88) (0.473)
S = 12,300 Combined Stresses using a strain concentration of 1.5 on the bending component S=2 (112,000/2) 2 + (12,300)
S = 115,000 psi.
Stress Range: = 115,000, Salt = 57,500 psi' E
N = 10,000 cycles O
n-2 Ag g c o,,,,
-20
' M vmb 1.6.1.3 Stress Calculations The purpose of this section is to present stress calculations caused by thermal gradients, pres-sure and mechanical loads for the maximum normal operating conditions.
There are no significant thermal gradients or limiting mechanical loads, pressure is the only item to consider.
During loading conditions, the cask is loaded with the contents at 100F.
With the cask closed i
and operating at the higher temperature con-dition, the average temperature of the air in the cavity will be less than 200*F.
Using 4
the ideal gas law, the internal pressure will rise from 14.7 psia to 17.3 psia (See Ss:tdon 2 4.4).
Considering the inner shell as a pressure vessel, the primary membrane stress is:
S = pr/t = (2.6) (14)/0.625 = 58 psi.
Considering the bottom cavity plate as a simple supported plate by ignoring the support of the
[])
lead, the maximum stress is:
2 S=
(6) (0.206) pr /t2= (1.236) (2.6) (19 6)/2. 25=280 psi.
The closure lid will have even lower stresses, the closure bolts are designed to take 100 psig and, therefore, it is not necessary to calculate any other pressure stresses.
1.6.1.4 Comparison with Allowable Stresses The design stress intensity, Sm, for the primary containment vessel at 200'F is 20,000 psj, table 1.3-1.
This is much greater than the calculated shell primary membrane stress of 58 psi and the cavity bottom plate stress of 280 psi.
l i
t f
1-21 AN EFCO, INC.
ex Y')
'O 1.6.2 Cold During operation at -40*F there are no changes in the operating capability.
The contents are shipped in a dry condition and the heat transfer means is entirely passive and no liquids are i
involved.
Structural materials have adequate impact values at -40*F.
The only adverse effect occurs when the lead contracts and places the inner shell in compression.
This differential radial contraction will cycle from -40*F to 180*F.
The range of 220*F will produce inter-
~
ference stresses between the lead shield and the inner shell.
To be conservative, the radial interference and l
resulting pressure was calculated for one cycle from 600*F to -40*F.
This is about six times the naximum normal expected alternating stress, because the lead will cold flow and,thereforejew nemn stress should be zero.
1.6.2,j0old - An Ambient Temperature of -40*F in Still Air and Shade v
I)
shield and inner shell during cooling af ter pardag of lead results in compression of the inner shell.
l The analysis conservatively assumes a continuous cool-down from tie lead melt temperature for
[
a long period prior to exposure to a -40*F L
3 temperature.
During'this time some relaxaticn of the contact forces exerted by the lead can be expected.
The theoretical maximum contact l
pressure between the lead and inner shell is t
7 determined by: (1) l l
(1) Timoshenko,S. " Strength of Materials, Part II, Advanced Theory and Problems," third edition, Van Nostrand, 1956.
- O.
1-22 ANEFCO, INC.
C l
rC l
Theoretical Contact Pressure l
bbI
~
P
=
L p3 (1/E,)
b2+a2 2
2+b_
+
+
(1/E )
c cz - b' bz - az
~
~
i
{
where (4 - c/g) 4T= (6.5 x 10 6) (660) a = 14.00 in. (inner radius of inner shell) b = 14.62 in. (outer radius of inner shell) c = 18.12 in. (outer radius of lead shield) h3 =k=0.3 (Poisson's ratio) 4290 Pp3 =
q 1
328 + 214
+ 0.3
+1 214 + 196
- 0.3 2.5 328 - 214 29 214 - 196 Bb " 1 500 psi.
P 1
Actual Maximum Contact Pressure However the yield stress of lead is
[yPb=860 psi.
therefore, the maximum equivalent hydrostatic pressure the lead is capable of exerting on the steel shell is from Roark Case IC, P.
504:
Pb (C2-b2
)
P
=
max
( CZ + b2
)
P
= 860 (0.210) = 180 psi.
ANEFCO, INC.
t f.[ x qq.
k/
JCircumferential Membrane Stress - Inner Shell The circumferential membrane stress in the inner liner as a result of lead contraction is g'g = (180) (14.00)/(0.625)=4,030 psi 4 3Sm (60,000)
Critical Pressure - Inner Shell The critical pressure for elastic stability for the inner shell is from case 19b, p. 558, Roark:
(Et /LR)fl/ leg 2)3(t /R 2
2 2 0.25 P
= 0.807 where R = 14.00 in.;
L = 180 in.
t = 0.625 in.
from which Per = 824 psi.
and since 824)180 psi., the maximum possible lead contact pressure will not buckle the inner shell.
1.6.3 Pressure f
Assess the package for the effects of 0.5 atmosphere external pressure.
Primary Containment The effect of a reduced atmosphere is to increase the operating pressure differential by 7.5 psi.
This would increase the maximum normal operating pressure differential in the primary containment vessel from 2.7 psi to 10.2 psi.
Therefore, the primary membrane stress in the inner shell goes to 230 psi and in the cavity bottom plate the stress goes to 1,100 psi.
Fire Shield This component is assembled at 1 atm. and the general primary membrane stress in the wall due to a 7.5 psi, differential is:
S = PR/t = 800 psi ( Sm (20,000)
O 1-24 AN EFCQ, INC.
rD 1.6.4 Vibration The cask is mounted on supports which are structurally part of the transporting trailer.
Thus, vibration of the cask itself is considered to be that of a long, essentially uniform beam, simply supported near the ends.
Weight, W.
60,000lg.
Bending stiffness, EI @200'F 916 x 10 lb - in.
Span support, 145 in.
The cask bending stiffness was taken as only that of the outer shell.
The total package weight was also used in determining vibration frequency, although part of the cask extends beyond the 1
supports.
Thus, the calculated vibration fre-quency will be less than the actual frequency.
This is conservative since the calculated fre-quency will be closer to the lower vibration frequencies of transport vehicle than is actually the case.
]
Lowest vibration frequency of the cask in a bending j
mode is:*
En" I'l I IE
- 9A
E' f
= 69 Hz n
This natural frequer.cy is satisfactory for truck transport, since it is well above the low frequency range of truck suspension systems (1-20Hz).
1.6.5 Water Spray A heavy water spray on the packaging will not harn the packaging because it is constructed of stain-less steel.
In addition, no water will leak into the primary containment because of the bolted closure and seals.
The impact limiter canning is also water tight.
Therefore, the only possible effect will be to lower the cask' temperature.
1 0
- Harris and Crede, " Shock and Vibration Handbook,*
McGraw-Hill 1961.
I l-25 ANEFCO. INC.
g(m f
1.6.6 Free Drop One Foot Drop Requirement Normal Conditions of Transport The extent of damage to the impact limiters, as calculated in the following paragraphs, may in certain situations be considered objectionable.
In those cases, where damage exceeds that which is predicted in the following paragraphs correc-tive action will be taken to replace the damaged impact limiter.
1.6.6.1 One Foot End Drop From 1.7.1.1, the initial and peak load is 2.24 x 106 lbs. to start crushing the aluminum shell and the balsa.
The expected deformation of the balsa for a one (1) foot drop is:
60,000 lbs x_12.33 in. = 0.33 in.
2.24 x 100 lbs.
()
The deceleration force for a one (1) foot drop is:
2.24 x 106
= 37.3 g's 60,000 The 37.3g value is the same as for the 30 foot end drop for which the various elements of the cask were analyzed in section 1.7.1.1.
The results of these analysis showed the various cask elements did not suffer permanent deformation or damage.
An analysis of the drain tube is presented on the next page because it is analyzed differently for the 30 ft. drop.
There is no reduction in the effectiveness of the packaging as a result of the one foot end drop.
r i
I 1-26 ANEFCO, INC.
F e
i
'(m
- ()
Drain Tube Stresses l
Assume a uniformly loaded !3am, a 170 inch high lead column, over a 1-1/2 inch wide tube.
i L
Loading is: (1.500) (170) (0.41) (37.3)=3 900 lb/in.
F jof length r
This is equivalent to a lead pressure of 2,600 psi.
i Drain Dimensions Length
- 3.5 in.
C
- 0.750 in.
Wall
- 0.156 in.2 Area
- 0.660 in.
D e2+ia
- 0.151 in. 4 j
For fixed end beam, case 2d, p.100} tar;k 2
M = WL /12 1
MC/I = (3,900)(3.5)2(0.75)/(12)(0.151)
S
=
b
- ()
19,800 psi. (at end )
S
=
b End Shear i
10,300 psi.
V/A = (3,900) (3.5)/ (2) (0.660)
=
Radial Stress
)
S = -2,600 psi. (outside, top only) l Combined Stress i=2(19,800/2)2+ (10,300) )l/2 l
S i
1 = 28,600 psi (Sy (30,000)
S i
I i
i
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4 1-27 ANEFCO, INC.
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1.6.6.2 One Foot Side Drop As reported in the referenced sections, the crush distance is 2.0 inches as the peak "g's" are In the analysis of the 30 foot side drop, it wds shown that the various cask elements did not suffer permanent deformation or damage.
Therefore, the lower "g" load development by the one foot drop will not reduce the effectiveness of the package.
1.6.7 Corner Drop This requirement is not applicable.
1.6.8 Penetration The requirement stipulates that the cask must withstand the impact of a 13 lb., 1 1/4 inch diameter bar falling from a height of 40 inches on the most vulnerable part of the cask.
The most vulnerable region of the cask is the 0.25 inch thick aluminum plate canning of the impact limiters.
If the 6061-T6 aluminum plate is assumed perfectly rigid, the kinetic energy of the falling bar must be absorbed by the shear deformation of the plate.
This is conservative because any bending defor-mation of the plate will also absorb energy and reduce the tendency for shear failure.
The energy required to cause shear can be expressed as:
2 K TF Dt gg E
=
5 where K = ductility factor = 0.11 S, = Ultimate strength in shear 27,000 psi O
1-28 ANEPCO, INC.
=
l l
e D = Bar diameter = 1.25 inch.
t = Plate thickness = 0.25 inch l
Thus the energy which the aluminum plate can absorb before the bar will produce shear-failure i
is:
KE = 730 in. Ib.
4 The kinetic energy of the falling bar is:
i' E
~
~
b r,
Thus the most vulnerable part of the cask will
,l not be penetrated by the falling bar.
hO J.
i l
1
!, O 1-29 l
ANEPCO, INC.
[M
~
j Stress in the Closure Shield Inner Plate Y = 13 in.,
t = 1.5 in.,
Im = 13.44 in.
i P=
(60) (0. 41) (1. 5) = 37 psi.
Treat as a simply support plate, subject to a uniform pressure of 37 psi.
f Moment at the center, Roark, Case 10a, p.363 M = 0.206 pr2 = l 400 in-lb/in.
j Maximum bending stress at the center S = 6M/t
= 3,700 psi.41.5 Sm (30,000 psi)
Stresses in the Cavity Bottom Plate and Botton Shield Intermediate Plate The 10,000 lb contents will produce a relatively uniform prc.ssure on the cavity bottom plate, which will then compress the lead in the bottom shield and thus load the intermediate support plate.
Both plates will have the same deflection shape O-and will act as two springs in parallel.
For simply supported plate, case 10a, p. 363, Roark 2
M
= 0.206 pr 2
S = 6M/t To determine the load that just produces yielding in the outer fibers, set S equal Sy (static).
2 2
p = St / (1.236) (r ) = (30,000)(2.25)/(1.236)(169) p = 323 psi.
F = pA = (323)(532) = 172,000 lb.
O 1-30 ANEPCO, INC.
ln()
Considering two plates, the total elastic load is 344,000 lb.
1 The load to produce a fully plastic hinge is twice the elastic load (1), ignoring any strain hardening effects.
This then raises the load capacity to these two plates to 688,000 lb., which is greater than the 600,000 design load.
Lead Slump Based on the information presented in ORNL-68,
- p. 63, the predicted lead slump for a cask with i
no energy absorbers is obtained from:
6H = RWH/3.14 (R2 - r ) (t, S, + RSp3) f 2
l l
where i
J R = 18.1 in. (outside lead radius) i f
l r = 14.6 in. (inside lead radius)
W = 60,000 lb. (package weight) t, = 1.5 in. (outer shell thickness)
S, = 50,000 psi (dynamic yield of steel)
S
= 5,000 psi (effective yield of lead)
I AH= (18.1)(60,000)(360)/3/14(115)(165,500) i A H = 6.5 inches j
4, However, the cask has impact limiters and the maximum l
laoding will be less than 60 g's.
From ORNL-TM-1312, j
Vol. 13, it was calculated that a 60 g loading will 4
l produce a lead slump equal to 40% of the unbuffered slump (1:7.5 model of Hallam Cask).
Based on these i
results a predicted lead slump of 3 inches was used.
This isless than the distance from the bottom of I
r the closure ring to the bottom of the closure inter-I mediate support plate and the distance between the bottom plate and the top of the aluminum insert e
Drain See Section 1.6.'6
()
l (1) Save and Massonnet," Plastic Analysis and Design of Plate, Shells and Disks," American Elsevier Publishing Co.,Inc.
N.Y.,
1972 l
ANEFCO, INC.
1-31
7
~S 1.7.0 Bypothetical Accident conditions The cask package consists of the cask proper with the addition of two detachable knergy absorbing limiters at the end.
Thest serve l
to protect the cask in the several attitudes of the required 30 foot free fall.
The bulk of the crushable material is great enough to allow complete energy absorption without striking through into contact with the cask.
The average and maximum accelerationt are lower than the design accelerations.
Protection against puncture is provided by a thicker than required outer shell and two 3-1/2 inch steel flat plate ends.
i I
Insulation against the fire accident is accom- '
plished by the stainless steel fire shield and air gap, and the inner skin of the impact i
limiters.
i 1.7.1 Free Drop
'[]}
Description'of Impact Limiters Reference ANEFCO, INC. Drawing No. SC 110.
f Both the top and bottom impact limiters are j
cylinders composed of three independent balsa wood structures, Zonas A, B and C, totally j
enclosed and hermetically sealed in aluminum canning.
The two impact limiters are inter-changeable.
l The external metal canning surfaces for the balsa wood structure is fabricated of 0.25 inch thick aluminum alloy plate (6061-T6)..The internal energy absorbing material is balsa, g
so oriented in each of the three balsa wood structures, as to present nominal end grain l
to the direction of crushing.
O 1-32 ANEPCO, INC.
i
'T Q
.1.7.1 Free Drop (continued)
A 1/8 inch thick asbestos sheet separates the balsa wood and the.altuninum canning which fits over the end of the cask.
This asbestos sheet serves as an additional non-combustable thermal insulator should the balsa wood be destroyed under the accident conditions.
A_gtachment of Impact Limiters to Cask The impact limiters are assembled and dis-assembled by sliding axially along.the cask ends into an extreme position where the bottom plate of the central palsa cylinder contacts either the bottom of the cask or the top of the closure assembly.
i In these positions the impact limiters are retained from axial motion by six 3/4 inch bolts O
which pull a threaded block inside the balsa shell toward a radial lug on the cask, the bolts being parallel to the cask.
The bolts have only a nominal function, since they are not' subjected to dynamic loadings in any drop attitude.
Consequently, convenience and operational considerations govern the design.
j Balsa Wood Properties F
The balsa wood density used in the impact limiters is eleven (11) pounds per cubic foot, with a comprehencive strength parallel to the grain is 1910 pounds per inch square peak. (Ref. 1) j J
Balsa wood, when subjected to end grain com-i pression testing, displays an early maximun stress, after a slight initial " bedding in".
l Further compression, to an average maximum of 85% of its initial height shows practically a l
l ()
Ref. 1:
Balsa Ecuador Lumber Corporation Data Sheet No. 70, 1963.
l-33 ANEFCO, INC.
i".s))
k Balsa Wood Properties _ (continued) straight line fall-off in stress through a point representing 30% reduction in stress at 754 penetration, extrapolating to 40% reduction at(Ref. 2) nominal 100% penetration. - See Figure The initial condition of the balsa wood impact limiters is maintained by treating the wood surfac~e with Woodlife, a wood preservative manu-factured by U.S. Plywood.
This particular pro-duct also meets the Federal Standard TTW-572B, which deals with the requirements of wood pre-servatives.
There is no indication that balsa wood is effected by aging.
The wood preservative, which is applied to the surf ace of the wood impact limiters, will provide an effective barrier to aging.
Additional protection against moisture and agi'ng is the encapsulation of the balsa wood in a hermetic aluminum enclosure.
Thus, it is not necessary to degrade the properties of balsa wood in the calculations for temperature, humidity or aging effects.
(
,,,...,=<=,i,;c:.
1-24 l
C
,~O Balsa Wood Properties (continued) t-
- --_ ~
2400 f
-5TERill7ED f
f-- DRY
{
g
/V j
~
g
^: g s.
l-kgy
'm.
-- QfN &
~
900 (X) = END OF USEFUL
~
600 ENERGY DISSIPATION 300 RAM SPEED = 1 in./ min l
I o
2J 0
9.20 0.40 0.60 0.80 1.00 1.20 1.40 1.60 1.80 2.00 2.20 2.40 2.60 2.80 3.00 RAM PENETRATIOP4 in.
O Ref. 2: Jet Propulsion Labortory Report No. 32-1295.
1-35
O 1.7.d.l.
End Drop This section considers the'deceleratihn and resulting stresses in the cask cover plate, top flange, bottom plate and cask wal;ls for the cask falling 30 feet and impacting on the top end.
The balsa wood in the upper impact limiter is crushed over an area equal to the top flange.
The total thickness of balsa wood is sufficient to sustain 75 percent deformation from the total energy absorption of the one foot fall and~the 30 foot fall.
1.7.1.1.1 Impact Limiters In as much as both impact limiters and the two g
ends of the cask are the same, the analysis of the deformation and the deceleration forces for both the bottom and the top end drop are the same.
In either drop attitude, only that portion of the balsa wood energy absorbing material shown as Zone A is effective in absorbing the impact energy.
~
, /
[-q...-
.. C
--- Sc2=
s 6
CASK AND ENERGY IMPACT ABSGRBER O
')
l-36 ANEFCO, INC.
,~
0i
f Deceleration t
Cask Weight (W) = 60,000 lbs.
Total Drop Height (H ) = 360 in. + bhlsa deformation T
By trial and error, the balsa deformation = 10.8 in.
H
= 360 in. + 10.8 inc. = 370.8 in.
T Peak stress for balsa deformation (
) = 1910 psi /in.
Diameter of Cask (D) = 39.25 in.
Effective Area of balsa deformation (A Zone A)
T (39.25)2 = 1210 in.2 A
=
Zone A 4
[p A Peak force =
Zone A B
where F is load required to cause failure O
B of restraining aluminum canning supporting Zone B and Zone C.
Bending of inner plate. 'F, 1MPACT UMITER ALUMINUM C#4NING 2
~
Assume ring, fixed at inner edge, concentrated load at the end.
O 1-37 ANEFCO, INC.
l q
~
l\\
Deceleration (continued) l
//
FORCE
(_
r r 20' es 4E' 2
S = 6M/t M = WL S limit = 50,000 psi M limit = St /6 = (50,000) (0.25)2/6 l
2 M = 520 in. - lb/in O
W = M/22 = 1b/1 24 I
cire = Tf D Force = (7) (84) (24) = 6,300 lb Multiply by 2 for failure F
13,000 lb B
Peak Force = 1910 x 1210.+ 13,000 Dece1eration Force (g) = Peak Force W
38.7 g's I
g = 2324100
=
60,000 g
O 1-38 ANEFCO, INC.
l
\\
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)
Deformation - Balsa cylinder, Eone A m
l Balsa content is 39.25 in diameter and 21 in. deep Area =.785 (39.25)2 = 1210 in.2 By trial and error, penetration depth is 10.8 in.
Percent of balsa crushed = 10.8_= 51.4%
21 Peak Stress = 1910 psi /in.
Final Stress = 1910 -
51.4 (764) = 1910 - 392 = 1518 1910 + 1518 = 1714 psi /in.
Mean Stress =
2 Energy absorbed in balga = 1714 x 1210 x 10.8 = 22,398.5521b.
Kinetic Energy to be absorbed.
60,000 x 270.8 = 22,248.000 lb/in.
Support for Inner Surfaces of End Impact Cylinders
([)
At the bottom of the cask, the 39.25 inch diameter base plate is directly supported by the cask bottom plate.
At the top of the cask, direct contact is nade on the 39.25 inch diameter closure lid, which in turn is mounted on the closure ring of the cask proper.
6 O
4 1-39 ANEFCO, INC. '
-=-
O
~
s.
- 2. 7.1.1.2 End Drop - Components Bottom Drop The bottom impact produces a 38.7g f.oading (See Section 1.7.1.1.1) on all components which is less than the 60g design loading.
This section contains stress calculations based on the 60g design loading.
S_ tress in Closure Shield Support Ring The lead shield and stainless steel plates weigh less than 1,000 lb.
P = 13 in.,
t = 1.0 in, A=81 in.2 S
= NgW/A = (60) (1,000)/81 = 740 psi. (Sm (20,000)
I O
I l
l
()
l-40 ANEFCO, INC.
I
./'t i
5I / \\
MJ 1.7.1.1.2 End Drop-Components (continued)
Top Drop Closure Shield Intermediate Plate and Inner Plate These are identical to the bottom shield interme-diate plate and cavity bottom plate.
Based on a assuming these plates as simply supported, the calculated results are the same.
Closure Support Ring R = 14 in.
t = 1.0 in.
A = 88 in S = 600,000/88 = 6,800 psi 4Sy (30,000)
The buckling stress is over 250,000 psi.
Cavity Bottom Plate The bottom shield is supported by the cavity bottom plate which is welded to the inner shell.
There will be some support of the bottom shield
' C) by the lead annulus, but for calculation purposes it was assumed that the bottom shield is free to move and is supported only by the cavity bottom plate.
r = 13.0, t = 1.5, 60 g loading, 3 inches of lead.
for a simply supported plate M=
(0.206) (73.8) (169) = 2,600 in-lb/in.
S=
(6) (2,600)/2.25 = 7,000 psi <[Sy (30,000)
Inner Shell 2
r,= 14.31, t = o.625 in., A = 56.2 in Compressive stress for a lead plug weight of 650 lbs.
and a bottom plate weight of 167 lbs.
S=
(60) (817)/$6.2) = 870 psi (Sm (20,000)
O 1-41 ANEFCO, INC.
P.K)
Buckling Stress Case 15, p.
555, Roark r/t = 22 L = 1.72 (rt)1/2 = 5.4 in. (less than 180 in.)
for S = 0.3, use 40% of theoretical load 6
S = 0.243 (29 x 10 ) (0.625/14.31) = 308,000 psi This is much more than the actual stress of 870 psi produced by the 60 g's acting on the bottom shield and cavity bottom plate.
Bolts The top end drop produces a shock loading on the 10,000 pound load and the 2,500 pound closure assembly.
Ignore the counter pressure of the balsa wood and assume the full design shock load on the 20 1-1/2 inch
-12 UHF closure bolts holding down the lid. (primary containment
.O internal pressure load is small).
1.5 x 100-lbs.
(120)(12,500)
F
= 2Ng (W)
=
=
W 6
S=
(1.5 x 10 )/(20) (1.52) = 49,000 psi (S (105,000)
)
1-42 ANEFCO, INC.
(~T y,)
[
(_
1.7.1.2.
Side Drop 1.7.1.2.1.
Impact Limiters Calculations of crush distances and deceleration forces using mean strengths of balsh is deter-mined in 1.7.1.2.2.
Only that portion of the Impact Limiters shown as Zone C in Figure 1-is effective in absorbir.g the kinetic energy of the side impact as the force required to
~
deform the aluminum canning around tone B offers neglible resistance compared to the crushing strength of Zone C Top and Bottom Balsa,Annslus - 30 Foot Drop __
Annulus Thickness = 15 in.
()
h = 11. 9 in. d = 41. 4 - 11. 9 = 2 9. 7 i.n n,
U Cox {}~ = 2 9. 7 =. 714 = 4 4. 4 e-Ey "U
Sin dy'= 0.70 a = R Sin d}' = 29.12 Side Area = 2 x 44.4 x
x 41.62-0 E
360" O. a (29.12 x 29.7)
- 477.4 in.2 Lg CRUSH DISTANCE' vol. Avail. = 15 x 474.4 = 7161 in.3 Contract Area A-A = 2 x 29.12 x 15 = 873.6 in.2 Final Forces on A-A = 1436.2 psi mean times as determined in Section 1.7.1.2;2 (1436. 2)M 873. 6) - 1,254,664 Final Peak g's = 1,254,664 = 41.8 g's 30,000 O
1-43 ANEPCD. INC.
f i
i Calculation of Mean Psi for Balsa Side Crushing f
1 i
ax = radial 1004 thickness of balsa i
ab = radial crush dist. Tactual max.)
'g 4 I
% of crush on conter radius = ab X
E f
i (for point b)
Pe 5
t a
j x
\\ \\ W N
MF" l
l 7
ab
= 11.9" l
ax
= 21. 0
j e max = 44.4 0
L
% of crush on 9 impact point = g etc. etc.
Q ax Stress at any point a,c,e,g,j, and 1 is S = (1910 psi)
I cos 6 for that point j
l Stress at any point, b,d,f,h,k, is derived as shown now
[
for point di Sd = (stress at c) - g (764) ax i,
l l
l l
Top Balsa. Annulus
- 41.6R
- 20.6R
- 30 ft. drop O
ax = 21 ab = 11.9 crush t
- i at point 4. stress
= 1910 psi.
l k.
= 1910 - 11.9 x 764 = 1487.3 l
D mean ab
= 1698,7 i
O P
1-44 ANEFCO, INC.;
- W m
c.
(1910) oos 9'
= 1886.5 d.
1886.5 - 11.4 x 764 = 1481.5 21 mean cd
= 1684.0 i
e.
(1910) cos 18
= 1816.6 f.
1916.6 - 9.9 x 764 = 1464.9 21
)
mean af
= 1640.7 g.
(1910) cos 27
= 1701.8 h.
1701.8
- 7.37 x 764
= 1440.0 21 mean gh
= 1570.9 j.
(1910) cos 36
= 1545.2 k.
1545.2 - 3.96 x 764
= 1404.5 21.25
(])
mean jk
= 1474.8 1.
(1910) cos 44.4 = 1364.7 Mean at impact line BB is b + 2d + 2f = 2h + 2K + 21 = 1436.2 psi.
11 Mean of whole vol. crushed is ab + 2cd + 2ef + 2gh + 2ik + 21 =
11 f560.8 psi.
0 1-45 l
ANEFCO, INC.
I i
i l
Top and Bottom Balsa Annulus - One Foot Dron h = 2.0 d = 39.6 cos 6 = 39.6 =.952
() = 17.84 4
i 41.6 4
sin d) = 0.306 a = R sin d) = 12.73 l
side area = 2 x17.84 (1741.6) -(12.73 x 39.6) =
l 360 i
2 538.8 - 564.1 = 34.7 in vol. 15 (34.7) = 521 in.3 "available" Vol. Reg ' d. = (12 + 2. 0) (60,000)
= 445 in.3 1846 Contact qxea = 2 x 12,73 x 15.0 = 381.9 in.2 Final fozco = 1828.4 psi mean) 381.9 = 698,265 l
()
Peak g's =
698,265
= 11.6 g's 60,000 Calculation of Mean Psi.for Balsa Side Crushing - One Foot Drog Bottom be.ls: annulus 41.6R a-x = 21.0 a-b = 2.0" crush a
1910 b
1910
'2.0 x 740 = 1840 mean a b = 1875 21 c
1867 d
1807 - 1.51 x 740 = 1833 tean c d = 1860 T
t l
e 1818
($)
t 1
f l-46 ANEFCO, INC.:
e I
- O
~
Mean at impact line cc is:
e
. + 2 (1818)
= 1828.4 1840 + 2 (1833) c 5
i Mean of whole vol is:
4 3875 + 2 (1860) + 2 (1818)
= 1846 s
I i
(
i t
i t
i e
1
'l O
1-47 ANEFCO, INC.,'
np) 1.7.1.2.2 Side Drop - Components
(_
Closure Shield Support Ring r
= 13 in.,
t = 1. 0 in.,
A = 85 in I = 7,736 in.
L = 11 in.
Shield and plate weight = 1,000 lbs.
Moment = (1,000)(60)(11) = 660,000 in-lb.
S = MC/7.= (660,000) (14)/7,736 = 1,200 psi.
Shear Stress = (1,000) (60)/85 = 710 psi.
Therefore, the combined stresses are much less than the allowable value of 30,000 psi Outer Shell The maximum stresses in the outer fiber of the shell produced by the dynamic loading can be obtained by ratio from the results of part 1 5.1 where the beam load of 5g's was calculated.-
However, for this analysis the strength of the inner shell is included because of the support of the lead which will force the inner shell to deform in the
/^3 same shape as the outer shell.
V S = 60 WLC/8I I = 31,600 + 5,800 = 37,400 in.4 S=
(60)(60,000)(190)(19.6)/8(37,400)
(dynamic) (50,000)
S = 44,800 psi (Sy It shall be noted that even if the outer fibers reach yield, the outer shell will not fail.
If one were to assume no strain hardening and a yield stress of 50,000 psi., there would be a reserve of 50% in terms of the load required to produce a fully plastic hinge.
mV l-48 ANEFCO, INC.
Closure Shield Lid and CJosure Ring A side drop will produce forces on the closure shield lid due to the acceleration of the lid and the force on the closure shield.
Assuming that the lid can move sideways, it will strike up against the closure ring.
The bolts will not be subjected to loading because the clearance between the lid and closure ring (0.045 to 0.C,65 in) is less than the clearance between the bolts and the lid holes (0.075 in).
The total closure assembly weighs less than 2,500 lb.
At a 60 g side load, the total bearing load is 150,000 lb.
Taken over the 3.5 inch depth of the closure ring, the load is equal to 42,900 lb/in.
From case 2C, p.517, Roark, the formula for a cylinder in a cylindrical socket is:
g = 0.591 (pE/K )
D K
= D D / (CD
-D) = (28.035) (27.970)/(28.035 -
y y
2 l
27.970) = 784.1/0.065 K
D 6
1/2 (c = 0.591 (42,900) (29 x 10 )/12,000
('c = 6,000 psi., which is acceptable O
l-49 ANEFCO, INC.
i t
O l
,q V
1.7.1.3 C_orner Drop, Top and Bottom The possible point of contact on1he impact limiter for this test falls on a circle with a' diameter of 39.25 inches.
This circle is identified by the diameter marked as AA in the following figure l
l i
CASK
%"ro C.G.
D c
c
@3-3().
=
2
~a J
4 I
- e
_1_
~
I~~-
3 4!
c W
!e
{ _.
c.sd \\F 9,g pAXIAL A-A Cask and Impact Limiter, Corner Drop Tests.
Zone B and C as shown are not effective in. absorption of energy as these two Zones are not supported except for the aluminum canning, which yields as previously determined in Section 1.7.1.1.1.
- O 1-50 ANEPCO INC.
i I
(7%
Corner Impact
'(])
Impact angle measured the corner of wood 8 = are tan 19.625 = are tan.169 = 9.6' 116 cos 9 = 0.986 2
Area normal to axis =.785 (39.25)2 = 1210 in
)
Crushing on corner impact to line b-g is equi-valent to crushing on bottom impact to line b-f, piready calculated, in regard to total energy absorption.
Th e initial peak "g" load is however deve-loped gradually and is slightly less than in the hattom drop.
impact is critical The bottom (or top)
~
rather than the corner impact inpoint of peak g's.
The mean deformation of 10.8 inches at the I
center line is the same as for direct end l
The peak value is generated along impact.
line d-e, where the mean stress is found
(])
from deformation e-a, or I
3.27 _ = 16.7%, which gives a stress 16.625 of S = 1910 (.167) 764 = 1782 psi peak 1782 (1210) + 13,000 = 36.2 g's Peak "g" value =
60,000 i
The extreme compaction occurs at point "g" on line b-g 10.8 + 6.54 = 17.3 0
17.3
= 82%
IITF 1
.This is less than the 85% at which the balsa begins to go solid, so the corner impact condition is without any non-linear behavior.
I A
($)
i 1-51 l
ANEFCO, INCd l
\\
hr%
1.7.1.3.2 components (Cover Drop)
The acceleration due to the corner drop,is 36 g's which is less than the vertical design load of 60 g's.
Since the critical angle is 9.6, a corner force of 60 g's (which is more than pre-dicted) produces a vertical force of 59 g's and a horizontal force of 10 g's.
This will produce much lower stresses than the side drop for the
)
closure shield support ring, outer shell and closure lid and ring.
For the other components, the stresses will be almost the same as the end drop because the vertical component is almost equal.
The laterial strength of these components is many times greater than the vertical strength.
i i
. ([)
r
/
O l-52 4
ANEFCO INC.
1.7.1.4.
OBLIQUE DROP
- 1. 7.1. 4.1
- Impact ' Limiter An additional' drop was investigated due to the unique geometry of the impact lihiter (see figure below).
It will be shown that suf-ficient balsa is present to prevent " bottoming' of the limiter.
MF
(
t i
d /.
h f,,,,,n
,~ CASK MAIN SHELL,
~ ~ ~ ~ ~ " ' " " " '
v,,
F rz dcor oblique Angle Drop, Impact Limiter Defounation.
O 100-90-80-u70-b60-o
~
Ls.i 5%
i GRAIN ANGLE, DEG.
O
'NO NO NO NO NO 70 b
b i
I salsa Wood Energy Absorption Efficiency O
1-53 ANEFco, INC.
.m An analysis of the oblique drop must be taken into account, the fraction of energy absorbed at impact, plus that portion which causes rotation.
From appendix 1.10-2, the following equation determines the fraction of energy absorbed at impact after modification for an angle e to the horizontal 2
2 a bs = 1 - 3b (cos e)2/ (4b2+c) a where 190 in.
b
=
39 in.
c
=
g l
27 e
=
i g,= 414 a
The crushing strength of balsa at 18 (45 orie'n-tation of Balsa Wood
-27 ) from the preceding 0
figure (0 8) (1910) = 1,526 psi.
O V = E/ [
(0.41) (60,000) (372)/ 1,526
=
= 6,000 in.
Due to the complicated geometry involved, the volume crushed will be approximated by a volume of revolution, with an assumed radius of r = (r1 + r )/ 2 (cos e) 2
= (19.5 + 40.5) / 2 (. 89)
= 33.7 in.
Using this dimension for R in the following sketchy l
h C I p. - q _ __Jt
/,/ /.
6
'O Q.,.
30 P
3 I
D --+
f
\\
ANEFCO INC.
1-54 l
~ O the amount of balsa compressed becomes A = V/L where 2
- 1) / c s e = 23.6 in.
L=
(r
~#
A = 6,000/23.6 = 254 in.2 i
now
+^
~ ^tri sector rect
^ sector = 77 ]R2(2B/360) where l
B = arcsin (D/2R)
(])
= arcsin 39.25/2 (33.7) = arcsin 0.582
= 35.6 A
= 73~(33. 7)
[2x35.6) sector
[ 360
)
= 705 in.2 A
= 1/2 Dh where h = R cos 'B
= 33.7 cos (35.6) = 33.7 x 0.81 6
= 27.4 in.
i l
()
l-55 g
ANEFCO, INC.
l 1
'#D i
q-A
= 1/2 (39.25) (27.4) i tri
= 537.7 in.
Arect "
sector tri
~
= 254 - 705 + 537.7 in.
= 86.2 in.2 l
d
=R-h+A
/D rect cor
= 33.7 - 27.4,+ 86.2
= 33.7 - 27.4 + 2.2 39.25
= 8.5 in.
O The maximum area available for crushing in this oblique drop is given by the same expression as used in the side drop analysis:
tri +
(~!'
A,,x = Asector
~
= 705 - 537.7 + 39.25 (27.4 - 39.25 )
2
= 472.5 in.2 A,y,y = 0. 7 5 ( A,,,)
= 0.75 (472.5)
= 354.4 in.2
'O c.
1-56 ANEFCO INC.
II)
Since this is greater than A = 254 ih.2 required to absorb the 30 foot corner drop, the cask is protected.
Note that adjoining regions of balsa were conservatively neglected in thik analysis.
1.7.1.4.2 components (oblique Drop)
As the impact area on the oblique drop is less than the impact area on the end drop, the peak of loading for the oblique drop will be less than the peak of loading for the end drop.
Using the peak of lor. ding for the end drop for the upper limit of the oblique drop, a value of 53.4 g's for the longitudinal component and 27.2 g's for the transverse component. Since each of these components is less than the design load of 60 g's, lower stresses occur in the closure shield support ring, outer shell and closure shield lid and ring than the 60 g siae load.
This occurs because these components are stronger in the vertical direction than in the side direction The re-maining components are much stronger in the side direction than the vertical direction and their stresses will be lower than those cal.culated for O
the end drop.
6 O
1-57
])
ANEFCO, INC.
A l.7.2, Puncture 1.7.2.1 Top Puncture Closure Bolts Assume that the 6 inch bar hits the center of the closure lid.
Calculate the stresses in the 20 closure bolts.
6 F = 1.4 x 10 lb.
force / bolt = 70,000 lbs S = 70,000/1.5 = 46,500 psi,cs (105 o00) j therefore, the bolts hold.
Assume that the pin load is at an edge of the lid This will reduce the load placed on the belts by
/3 the pin when compared to a central contact, but
( k/
will now cause a condition where the closure lid may try to rotate around one edge.' The loading on the bolts will be caused by the acceleration loading of the lid and contents i
O 1-58 ANEFCO, INC.
(7 :
6 The maximum pin force is equal to 1.41 x 10 lb.
This will produce a maximum acceleration of:
6 (1.41 x 10 )/60,000 = 23.5 g.
N
=
f Assume that because of the rotation of the lid the effective restraining force is equal to only half of the bolts.
With a 2,500 pound closure assembly and 10,000 pound load, the bolt stress is:
S = N W = 23.5 (12,500)/(10)(1.52) 9 S = 19,325 psi <Sy (105,000)
Closure Lid The lid is made of a 3.5 inch thick plate bolted to the closure ring.
Assune that the punch strikes the center of the lid.
For this analysis, the re-mainder of the closure assembly is ignored.
Elastic Phase Simply supported flat plate, case 16, p. 367, Roark.
The maximum load for which the plate remains elastic Os is one that just produces yield in the outer plate fibers due to bending.
At the center, the moment Fi
=M r
t max (6W/4[t )((1 +h) 2 S
6M/t2
in (R/a) + 1) where R=14in.,a=3'in.,h=0.3 Sy = 50,000 psi.
2 W
= 0.698 St (gy)
Y y
W = 427,000 lb.
Y The deflection is given as:
Y
= -WR /16T D (3 + N )/(1 + h )
2 c
where D = Et /12 (1 h 2) 3 O
~'
ANEFCO, INC.
r ~.
Y
= 0. 239 WR2 (1 -
) (3 + 9 )/Et3'
(
e t
where 6
t = 3. 5 in, E = 29 x 10 psi.
Y
= 108W/Et3 (S2)
C Y
= 0.037 in.
c The kinetic energy absorbed by the elastic defor-mation is negligible.
Elastic to Fully Plastic Phase From p. 126 of Save and Massonnet the collapse load is:
(t /4) (S,) (6M(3-2a/R) 2 W
=
u 2
W
= 1.84 S t W
= 92,000 t2 = 1,127,000 lbs.
Assume that during the transition from the elastic to the fully plastic phase, the deflection rela-tionship is governed by the elastic relationship.
s This will predict less absorption of kinetic energy than actual and will leave more kinetic energy to be absorbed during the fully plastic phase.
This will also result in larger predicted deflections.
6 Mean Load = (1.12 7 + 0. 4 27 ) 10 /2 = 777,000_lb.
Deflection = (777) (0.037)/427 = 0.067 in.
KE2= (0.5)(777,000) (0.067) = 26,000 in/lb.
Fully Plastic Phase The total amount of kinetic energy to be absorbed for estimated final distortion of 3.0 inches is:
0 (60,000)(43) in/lb. = 2.58 x 10 in/lb.
KE
=
l i
O 1-60 ANEFCO, INC.
t
-y l
pV The kinetic energy absorbed by both the elastic and elastic-plastic transition phase is negli-gible.
Therefore, the. total kinetic. energy is to be absorbed during the fully plastic' phase.
Plastic deformation = 2.58 x 106 = 2.29 in.
1.127 x 100 Total deformation = 2.4 inches Ductility Evaluations The extension of the extrece fiber on the bottom of the plate at its center can be represented by the sum of two separate extensions.
[l
= elongation of the neutral axis as the plate is bent.
This is a " membrane stretch" and is assumed to be applied to the botton extreme fiber as well as the neutral axis.
[1,=elongationofthe trene bottom fiber for the neutral axis, beyond that calculated as 11 due to the plastic hinge.
O ThA lg
.I_
I F h/'
157 5 -
A i
& 8f a
~
ly = 14.0
+ 2.4
- 14.0 = 0.204 in.
[1 (2.4 ) (1.7 5) /14. 0 = 0. 3 00 in.
2=
[1 12 = 0.504 in on each face of,the plate.
1 For these dimensions (28" dia. x 3.5" thickness) a 7 inch gauge length is appropriate. On
~
his basis, elongation = (2) (0.504)/7 = 14.4%.
t O
ANEFCO, lNC.
1-61
r-
~t(m_)
The angle of bend of the plastic hinge which results j
is:
E)E (625/2) = 2.4/14.0 - 0.171 435/2 = 9.7*
(E) = 19.4* of bend which is O
satisfactory for this material material.
Examining the ductility ratio, the available " ductility ratio" = 40%
= 200 0.2%
4 where 40% elongation is the minimum for T ype' 304.
The used
" ductility ratio is 14.4/0.2 = 72 MS = (200/72)-1 = 1.78 Considering the ratio of final deflection =
2.40
= 65 elastic deflection
.037 This may be roughly related to the above ratio of 200 "available".
Shear at the punch contact Perimeter of Pin = 67 finches Area of plate in shear = 3.5 (6 7[') = 65.9 in.
~
6 lbs.
Collapse load = 1.127 x 10 S, = 16,400 psi <( 0. 6 Sy (18,000)
The safety margin is actually much larger because the 18,000 psi, limit is a' design criterion to prevent the onset of shear.
It would really take a force equevalent to a 57,000 psi. shear stress to puncture the plate (Marks, Table 2, p. 13-25).
O P
.I 1-62 ANEFCO, INC.
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'i
1 n
l.7.2.2 Bottom Puncture Assume punch hits center of bottom Punch force 1.41 x 106 lb.
Punch pressure (max) 50,000 psi.
Stress in Outer Shell 2
1 f
= 18.9; A = 178 in 2
lb)/(178 in ) = 7,900 psi S = F/A = (1.41 x 106 Buckling Stress is (case 15a, p. 555 of Roark) s = 0.3 Et/fi = 600,000 psi.
therefore, the outer shell will,not buckle.
BottomPlate The bottom of the cask is made of a 3.5 inch thick plate welded to the outer shell.
The i
internal structure welded to the plate has been ignored for this analysis.
i Plastic Phase l
For a simply supported flat plate, case 16, p.367, Roark, the maximum load for which the plate remains elastic is the one that just produces yield in the outer plate fibers due to bending.
At the center the moment M =Mt"N
.i r
max l
6M/t
= 6W /4 7 t fl+ 'h)
I 2
in (R/a) + 1)
S
=
y y
where:
R = 18 in, a = 3 in., t = 3.5,'N= 0.3 2
0.629 S t (31) i W
=
y y
i, 385,000 lb.
W
=
4 y
7 The deflection is given as:
2 4
- (WR /167f D) (3 +N) / (1 + h 2
Y
=
e
'O l
g 1-63 ANEFCO, INC.
i
~ t0 Y
= 0.239 WR2 ' (1 -1) ) (3 + 'h ) /Et c
3 Y
= 179W/Et (S2)
Y
= 0.055 in.
c The kinetic energy absorbed by the elastic deformation is negligible.
Elastic to Fully Plastic Phase From p. 126 of Save and Massonnet the collapse load is:
(t /4) (S ) (67/(3 - 2a/R) 2 W
=
y W
= 88,200 t2 = 1,080,000 lbs.
Assume that during the transition from the elastic to the fully plastic phase, the deflection is governed by the elastic relationship.
This will predict less absorption of kinetic energy than actual and will leave more kinetic energy to be absorbed during the fully plastic phase.
This O
will result in predicted deflections larger than actual.
6 Mean Load = (1. 08 + 0. 3 8) 10 /2 = 730,000 lb.
Deflection = (730) (0.055)/385 = 0.10 in.
EE2= (0.5)(730,000)(0.10) = 36,500 in/lb.-
Fully Plastic Phase The total amount of kinetic energy to be absorbed for an estimated final distortion of 3.0 inches is:
6 (60,000)(43) in/lb. = 2.58 x 10 in/lb.
KE
=
t l
5 V.
Y MUCD, WC.
l-64
This angle of bend of the plastic hinge which re-sults is:
arc tan (ep/2) = 2.54/18.0 = 0.141 d53/2 = 8' GE} = 16' of bend which is satisfactory for this material.
Examining the ductility ratio, The available " ductility ratio" = 40% = 200 0.2%
where 40% elongation is the minimum for type 304.
The used
" ductility ratio" is 12.1/0.2 = 60 Considering the ratio of final deflection = 2.54 =46 O.055 This may be roughly related to the above ratio of 200"available".
(}
Shear at pin contact e
Perimeter of Pin = 6 // inches Area of Plate in Shear = 3.5 (6Tl = 65.9 in.2 Collapse Load = 1.08 x 106 lbs.
S
= 16,4 00 psi. < 0. 6 S (18,000) s y
1.7.2.3 Side Puncture i
Outer Shell Bending The 40 inch drop onto the 6 inch diameter bar at the midsection of the cask represents the case of maximum bending moment into the cask.
The force exerted by the bar is:
Fp=(d Ap
[d 50,000 psi. (dynamic flow stress)
A
= 28.26 in.2 ( area of cylindrical bar) p 6
F
= 1.4 x 10 lb.
p 1-65 ANEFCO, INC.
P w
e f'N The kinetic energy absorbed by both the elastic b-}
and elastic-plastic transition phase is small so that all the remaining kinetic energy is to be absorbed during the fully plastic phase.
Plastic Deformation = 2.58 x 106 = 2.39 in.
1.08 x 100_
Total Deformation = 2.54 inches Ductility Evaluations The extension of the extreme fib er on the bottom of the plate and at its center can be [ represented by the sum of two separate extensions:
Li = elonge-tion of neutral axis as the plate is bent.
This is a " membrane stretch" and is assumed to be applied to the bottom extreme fiber as well as the neutral axis.
c[ l
= elongation of the extreme bottom fiber beyo$d that calculated as d$ 1 for the neutral axis 1
due to the plastic hinge.
4,-
O m
a = 's ef;,.
A
,I 1
4 3.5"
" bf i
i 1.75..
[
l
+
.L A
--bkg l
h1 (18.02 + 2.542) 1/2 - 18.0 = 0.178 in.
=
[1 (2. 54 ) (1.7 5)/18. 0 = 0. 247 in.
=
2 hly+[1 0.425 in on each face of the plate 2
For these dimensions (36" dia. x 3.5" thickness) a 7 inch guage length is appropriate. On this basis, elongation = (2) (0.425)/7 = 12.1%
i
()
1-66 ANEFCO, INC.
tT%
k)
Treating one-half of the cask as a cantilever beam with a uniform loading equal to one-half the bar force yields a maximum bending moment of:
(F /2) (L/4)
M
=
b where L = 200 in.
6 M
= 34.27 x 10 in/lbs.
b The maximum bending stress is:
S = M /I = 21,300 psi.< 1.5 S, (30,000) c Outer She?.1 Puncture The required thickness of the outer shell for cylinders having a diameter greater than 30 inches is determined by ORNL - 66.
R"
! uit t
'a where W = loaded cask weight, 60,000 lbs.
S
= ultimate tensile strength, 75,000 psi.
ult The calculated result is:
t
= 0.85 inches, g
which is less than the outer shell thickness of 1.5 inches.
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l.7.3 Thermal
- (d' 1.7.3.1 Summary of Pressures and Temperatures _
As a result of the hypothetical fire accident, the temperature and pressure of the primary containment are increased to about 475'F and 25 psia.
The lead shielding reaches 500*F and the outer shell has an average temperature of 550*F.
l.7.3.2 Differential Thermal Expansion The major problem caused by differential thermal expansion will be at the drain because of the 75'F difference in average temperature between the inner and outer shell.
The difference in axial growth is equal to:
T, 6 L =oc T g,s is os os i
AL= (180}}9. 76) (550-70)
- 9.62 (475 - 70) x 10
\\
fiL = 0.14 inches
)
Stresses caused by this differential thermal expansion do not have to be analyzed because there are no pressure loads on the drain tube and therefore, the stresses are self limiting.
In addition, no fatigue analysis is required because this is a one cycle event.
In the event that the drain tube parts, the primary containment will not be penetrated because the boundary seal is located in the drain i
housing.
l.7.3.3 Stress Calculations i-Stresses in the primary containment will be increased due to the rise in cavity temperature and pressure.
At a temperature of 500*F and 25 psia (11 psig) the primary membrane stresses are:
S = PR/t = (11) (14)/0.625 = 246 psi.
Cavity Bottom Plate Bending S = 1.236 pR /t2= (1.236)(11)(196)/0.391 S = 6,800 psi.
ANEFCO, INC.
f?
iv' l.7.3.4 Comparison with Allowable Stresses At a temperature of 600*F the allowable primary membrane stress is 15,600 psi. and the allowable membrane plus bending stress is 23,400 psi.
This is much higher than the stresses produced in the primary containment at the end of the hypothetical-fire accident.
It should be noted that the primary containment was designed to meet 600*F and 100 psig This l
is much more severe than the 500*F and 11 psig l
condition produced by the hypothetical fire accident.
- D 1
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1-69 ANEFCO. INC.
l F
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APPENDIX 1.10-1
.I CASK MASS MOMENT OF INERTIA J
f 4
A J
{
i q
C
~
1 j
l O
~
I I
=M (4b2+c)
This is for a solid bar.
i 2
H l
i 1
(Mech. Pt. II - Dynamics, Merian, p.
396, 1959)
However, cask is not solid but can be approximated as a square cask with a square hole in center:
s' 2
2 (M/12) (a /c ) (4b2+32)
I
= (M/12) (4b2+c) net where b = 190-in. (cask length) c = 39 in. (outher shell diameter) t a = 14 in. (cavity inner diameter).
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L ANEFCO INC.
1-70
,_~,v.
.,_..__.--y.
.- m iO Cask Mass Moment of Inertia (continued)
The term "a /c " in the above equation is needed to account for the mass in this region.
Sincg M denotes the mass in the rectangular prism "bc ",
it must be modified to account for mass in " hollow" rectangular prism.
2 M = pbc 2
2 M
= pb (c
-a) net 2
2 2
M=M C /(c -a )
et I2 I
=M
/12 c
4b2 +c2 22 4
net net
- 4a b
-a (c-a2 2
c#
2 j
/
c P
J l'= mvb (See Appendix 1.10-2, " Energy Transfer")
2 bet Conservation of energy:
2 (I
/2)' + U (mv /2)
=
net g
- where, U
= Energy absorbed at Point O (impact) g U
= mv / 2 - I f12/2 2
o net 2
= mv /2 - (I
/2) (mvb/2Inet)
{
net 2
222
= mv /2 - (m y b / 8Inet)
()
b l-71 ANEFCO, INC..
D.
Cask Mass Moment of Inertia (continued)
Substituting for I et
)
f2 2
[
(3){q.,_ g._
c a
2 2
2 my b
=
mv f
2 _ 4,2b ' -[
2 4b
+c i
\\
c c
2
~-
-)
i
= mv 2
2 (c _,2/c )
=K mv 2
2 1-3b 2
2 2 2 4
4b2+c
- 4a b
- a_
2 2
c c
i 2
I K=
1 - 3b (1 - a /c )
i 4b2+c2 22 4
- 4a b
-a c 2 7
C C
i Since "b" is much larger than "a" and "c", one may use:
K _~_ 1-0.75 = 0.25 1
1 o
i l
1-72 ANEPCO, INC.
4 i Q'.
- O APPENDIX 1.10-2 ENERGY TRANSFER i
Let point "O" (see Figure below) be the point of impact on the six-inch diameter bar.
V j'
a_
c y
l
]
d-6.0 Ma &
(
s 1
s y
~
~
By
~
1 b
<O i
HORIZONTAL-END IMPACT ON SIX-INCH BAR f
The initial angular momentum about "O" before impact is equal to the moment'of its linear momentum.
l i
H
= mvb, moment of linear momentum.
U 2
The angular momentum about "O" just after impact l
l when the cask is starting its rotation is:
If
=I A, angular momentum o
om O. = annular velocity.
l 1
Conservation of angular momentum requires mvb =
I fl 2
om I
f
- O 1-73 ANEPCO. INC..!
i
-.... ~,,., - -,. ~. -... -.... -... _. - -
i I
A Energy Transfer (continued)
I r
t where the mass moment of inertia of the cask about i
point "O" may be approximated by:
j t
2 I
= m_ ( 4b2+c),
g 12 j
when there is no central " hole" in the cask (See Appendix 1.10-1).
However, it can be seen that, in the final analysis, the dominatiing term is the cask length.
Consequently, an accurate description i
of the cask cross-section is a second order term and may be neglected.
Therefore, O. = mvb radians 21,
g D
f), = 12vb radians.
2, 2)
By conservation of energy, the kinetic energy immediately before impact equals the rotational energy plus the energy exchange at the impact point.
2 I
fL2 mv
=
om
+U g 2
2 U
= energy absorbed at point of imr.ict.
g Rearranging 2
20' = mv
-I
[12vb 2+c)}-
om
\\2 bb yields 2
2 U
= mv 1 - 3b_
n 2
(4b' + c')
1-74 ANEPCO, INC.
y
6 Energy Trasnfer (continued)
Let b = 190 in., cask length with impact limiter removed c = 39 in., outer shell diameter therefore, 2
U
= 0.26 mv o
2 i
Thus, the energy absorbed by the impact point is 0.26 times the kinetic energy of the cask.
The remainder of the kinetic energy is transferred into rotational energy about the point of impact.
Assuming the energy dissipated at impact goes into deforming the cask, the deformation energy of the cask is:
i 2
U
= 0.26 mv in 2
> O V
2 The kinetic energy mv is equal to the potential 2
energy (WH), where W = 60,000 lbs, cask weight E = 40 in., free fall distance.
I Therefore, the energy absorbed by deformation of the cask is:
U.
= 0.26 WH in (0.26) (60,000) (40)
U
=
1 6
U.
= 0.624 x 10 in.-lbs.
In 4
s i
O 1-75 AN EPCO, INC. -
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i i
Y3 2.0 THERMAL EVALUATION 2.1 Discussion i
l
_The packaging is designed to safely contain i
metalic non-fissile material under the required i
normal and accident conditions.
The thermal l
l analysis of the cask under the conditions out-lined in 10CFR71 is described in this section.
1 These conditions include: high and low ambient temperature, solar heat load, and the hypothe-tical-fire accident.
i The only thermal limitation on the cask contents i's that the maximum internal heat generation i
will not exceed 0.3 KW.
During the 130' F ambient temperature condition with full solar
['
load, a maximum internal temperature of 180*F
}
and.a pressure of 17.3 psia is expected. - This i
t l
is well below the 600*F and 115 psia design con-ditions for the primary containment.
The maximum surface temperature of the cask, for a 130*F
. ambient temperature, is 180*F.
This is equal to the 180*F maximum accessible surface temperature J.
allowed by regulation and, therefore, cask access will not be limited by a barrier during shipment.
1 I
j i
{
There are no fluids used in the cask, and there-j fore, the limiting cold condition is -40*F, no j
decay heat and no solar load.
The cask is designed to withstand the combined l
[
, drop, puncture and fire accident conditions i
l without releasing the primary internal cask coolant.
The cask is protected from the fire i
accident by an external fire shield.
The shield is made of 3/16" stainless steel with aui air gap 1,
of 0.100 in between the shield and.the outer shell.
i
?
j Calculations of the cask response to the hypothetical 1
fire accident indicate a maximum internal bulk' coolant.
l temperature below 500*F.
At this temperature con-
)
tents are below the normal operating temperature j
experienced during reactor operation.
i l
i l
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2-1 j
ANEPCO, INC.
(
P
.__,.._.w, ymr,cc,.._.-.,,,-.y,..__..--,-,--,...%,,,,,,.. -
,,,,,,.,,..m._,.-,y-y-,,,,.,---r
,-we
- ,w-..-
..y.
. - - - -, - -.--w
.m
- = -
t b
~ (i)
Thus, there is no danger that the contents
-will degrade as a result of the fire accident.
i The maximum internal cask pressure correspon-i ding to the calculated coolant temperature I
during the fire accident is 11 psig.
This is below the maximum internal design pressure j
of 100 psig.
Thus, the coolant, and any radioactive corrosion products will be re-tained in the cask under the fire accident.
l condition.
f I
The critical areas to model and determine temperatures were: the closure assembly seal, the bulk coolant temperature, the lead shield, and the drain plug seals.
l l
I 2.2 Summary of Thermal Properties of Materials i
The thermophysical pr6perties of the materials I
of construction of the cask are presented in
{
this section.
F For the Steady State Thermal Calculations
.{ )
(k= Btu /hr-ft *F; fCp= Btu /f t3 "F)
)
Material k
Cp Stainless Steel 11 54 l-l Lead 63 41 i
i Fire Shield Air Gap '(1) 0.233 1.08 1
i For the Transient Thermal Calculations l
4 f
I Material k
Cp I
I i
Stainless Steel 11 54 h
Lead 63 41-i Fire Shield Air Gap (1) 0.246' 1.08 i
Aluminum 119 36.2 i
Asbestos 0.13 9.0 i
Upper Aluminum Air Gap 0.104 0.14 j
Air Spaces in Closure l
. Assembly 2.85 0.14 I
i A (1) This is a volume weighted value assuming the t
iV the spacers, outer shell and fire shield remain l
in contact (see appendix 2.6).
E t
2-2 i
1 ANEFCO, INC.
l
r*.
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b 2
Lower Aluminum Air Gap (h= 11.5 But/hr-ft
- F)
Closure Assembly Air Gap (h = 11.5 Btu /hr-ft2
'F)
Outside of fire shield and asbestos (See figure 2.6-1) 2.3 Technical Specifications of Components This section contains a description of the technical specifications and limiting con-ditions of those components that would be affected by the temperature reached during the fire or whose perfe:mance would be com-promised by these high imperatures.
Two key items are the closure assembly and drain plug seals.
These seals are made from VITON with a continuous operating tem-perature limit of 400*F and a 48 hour5.555556e-4 days <br />0.0133 hours <br />7.936508e-5 weeks <br />1.8264e-5 months <br /> life at 600*F, See figure 2.3-1.
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ANEFCO, INC.
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1 VITON stays operational-from 400'F to -40'E l
and below i
Figure 1 shows service limits of VITON' in 10#~i otrr rE H
air at various temperatures. As evidenced
.P f
by the graph, VITON remains usefully HEAT RESISTANCE elastic for an indefinite period at temperatures up to 400'F. (204*C). These F
i
~
values become more meaningful when it is realized that most rubbers have a service
~
yyro hri temperature ceiling less than 250*F. (121'C).
M q
m A.t..
At high temperatures, VITON resists hea( %-,
Sp g d
_ >1000 hrs
,1 and simultaneously retains its good n
i mechanical properties better than any J
l
!O oiher eiasiemer risere 2 iiiesirates the s
effect of oven air aging on specific
[
mechanical properties of VITON, at j
i various temperatures over prolonged i
p-t periods. As the table indicates, VITON retains two thirds its tensile strength and i
3 elongation properties even after exposure
{
to 392*F. (200*C) air for 11 months.
ym,
,l i
a m
Seals of VITON can be designed forlow i
i j
'j 4
temperature service to give satisfactory sealing in dynamic applications down to f50*;
N
[*[
q.F.
W r.
-40'F. (-40'C). For static applications, 20cc.
232'c 26c'c.
2a:*C 315'c.
I it has been used at -65'F. (-54'C.) and TtsT 7turttATuats i
lower-down to cryogenic temperatures.
FIGURE 2.3-1 Heat Resistance of VITON.
Data from Dupont bulletin A-98591.
o 1
2-4
.4
.... = -.
4 1
e 2.4 Thermal Evaluation for Normal Conditions I
of Transport l
I The effects of the' normal thermal conditions l
of transport have been determined by analytical methods.
No model test will be made and.there 4
will be no thermal test of the bond between the lead and the shells.
The two extremes of thermal loading for the normal conditions are:
l i
(1) isothermal at-40*F; and, (2) a decay heat load of 0.3 KW with ambient air of 130*F and full solar load.
The bulk coolant in the cavity is air.
2.4.1 Analytical Thermal Model j
Because of the low internal heat generation 4
and the fact that non-fissile material is being j
handled, a thermal analysis of only a slice from the central section was performed using the THERMQS computer program, Section 2.6-2.
A review l
.)
of the THERMOS model is shown in figure 2.6-2.
This was a one dimensional steady state analysis.
a The internal heat generation was taken over a
[
](])
length of 144 inches resulting in 86 Btu /hr j
per foot of length.
l t
i The inside of the inner shell was assumed to be an adiabatic surface because the temperature r
drop to the contents would be negligible at i
these heat rates.
The lead interface with the i
i shells was assumed to have no contact resistance because the major drop is across the. fire shield air gap.
This resistance is much greater than l
.any reasonable value for the lead interface re-sistance.
j I
The fire shield gap was treated as a mixture l
of air and stainless steel with a volume weighted thermal conductivity of 0.233 Btu /hr - ft
'F.
1 I
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I i
t
+
i i
C:)
4 I
{
2-5 L
ANEPCO, INC.
i i
1 l
1 Y
(con't) t Analytical Thermal Model The solar load was assumed to be 144 Btu /hr per square foot of projected area, which results in a total heat input of 480 Btu /hr per foot of length.
Hand calculations were performed to compute the outside surface heat transfer coefficient, effective thermal conductivity of the air gap, j
and the cquivalent temperature rise for nodes 5 and 29 required for the THERMOS program.
i See section 2.6.3.
4
.i F
i j
i i
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2 v :,<
S Q !"b. ls
(
'l l
l E>
uw 2
l ses tc @
-- p a,
?;
w esz u 6 O
"3 Eit
=
9
-s
\\
'l I 8
\\
, eso*tt @
e
'N i
h
- O s
lh, 5
fil oss se @
- NN\\
In i
-n.
~
EF
~;.= i ju'Jr @
f a
t y
l 1
Q i
e o
2:
'l t
A
,\\
\\
i s2s te @-
,;\\
=
\\
H
/
0 g
1U O
Hc fN
=
Jt e It w g
l
, "v z
O N
J2t'oC 6 i /
\\
/ j#
l
^
=
32 9 'St Q
- / i //
eto ovesw t
9 i
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G G
G t
r l
8' O
o 4
s c
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0 a%
o e
4 4
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l l
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FIGURE 2. 6-2 One Dimensional Thermal Model for cask central region.
j h7
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)
2.4.2 Maximum Temperatures The temperature distribution within the cask under normal operating conditions is almost uniform in all material regions with the only significant temperature difference occurring between the surface of the fire shield and the ambient air.
The results at 130*F ambient temperature, 0.30 KW internal heat generation and full solar load, are:
Fire shield surface temperature 179'F Outer shield surface temperature 179'T Cavity boundary temperature 179'F 2.4.3 Minimum Temperatures t
This is the isothermal condition at - 40*F.
]
2.4.4 Maximum Internal Pressure The condition of maximum internal pressure occurs when the cavity bulk coolant is at
'-( )
its highest temperature.
This occurs during the condition of 130*F ambient temperature, full solar load and a decay heat of 0.30 KW.
Internal pressure will be a function of the 3
average temperature in the cavity.
Based on the results described in 2.4.2, the maximum inner shell temperature was 179'F.
To be conservative, a bulk temperature of j
200*F was used to calculate the maximum in-ternal pressure.
The initial loading tem-i perature was assumed to be 100*F.
PV = NRT l~
P2=T P /Ty= (660) (14.7)/560 1
P2 = 17.3 psia.
There will be no effects due to phase change, fluid expansion, gas generation or chemical decomposition.
l 0
2 ANEFCO, INC.
[
(Ik 2.4.5 Maximum Thermal Stresses Within the range of normal operating condi-tions, the worst combination of temperature distribution that occurs to produce therr a1 stresses, happens at the two extremes of operating conditions.
At the ambient condition of -40*F, no internal heat generation or solar load, the packaging is isothermal at -40*F.
This con-dition causes thermal stresses between the lead shield and the inner shell because of the greater contraction of the lead shield.
No other components have thermal stress pro-blems at the isothermal -40*F condition.
At the maximum temperature condition there may be some radial interference between the shells and the lead, but this would be equal to or less than the thermal stress produced at the cold condition.
The only other thernal problem may be caused by the higher tempera-ture of inner shell vis a vis the outer shell.
THERMOS calculations indicated a temperature difference of less than l'F.
To show that
(~N l'F is an upper limit, consider the heat kJ transferred across a 3.5 inch lead wall with a l'F temperature difference.
2 q = k (dt)/L ' (19.6) (l'F)/0.29f t = 67.6 Stu/hr-f t For a length of 12 feet and an inside diameter of 29 inches, the total heat transferred is 6,170 Etu/hr (1.8 KW).
This is six times greater than the actual decay heat load.
2.4.6 Evaluation of Package Performance for Normal Conditions of Transport The expected temperature range of the components is between -40*F to 180*F.
This is acceptable for the VITON seals.
No other materials or components have operating temperature limits in this range.
The thermal stresses are cal-culated in section 1.6.2 for the radial inter-ference and section 1.6.1 for the axial inter-forence.
OV !
i 2-9 AN EFCO, INC.
.A
O
-2.4.7 Thermal Evaluation of RH-TRU Canister The RH-TRU waste mat'erial that will be shipped will have-different decay heats associated with it.
For that reason evaluation was performed to evaluate the temperatures an that would prevail for total decay heat generation of 300 and 1000 watts per package.
2.4.7.1 Package Conditions and Environment It is assumed that in addition to the decay heat, the package is exposed to an environment of 100*F l
where the cask absorbs 400 cal /cm2 as specified in 10CFR71.71 under normal conditions.
{
2.4.7.2 Package Temperature Assuming the following thermo-physical properties of the materials of construction of the cask exist i
at steady state:-
1, Material k(BTU /hr-ft*F
!O Stainless Steel 11 Lead 63 I
Fire shield air gap 0.233 equilibrium Theatemperatures of the surface of the AP-101 cask, the temperature of the air in the AP-101 cask void, 2
and the tamperature of the proposed canister surfaces 1
were calculated assuming the ambient air temperature is 80*F.
Temperature (*F)
Decay Heat AP-101 Surface AP-101 Air Canister Surface 300w 82.3 92.4 98.1 1000w 89.4 120.3 140.1 Under the environmental conditions specified in 10CFR71.71 where the cask will be exposed for 12 2
hours to 400 cal /cm2 or 929 BTU /ft ' the maximum equilibrium temperatures increased by 69.l'F.
I O
2-9a Rev 2 - 4/1/86
- ()
2.4.7.3 Evaluation Summary i
The temperatures that will exist in the package were calculated above.
Under normal operating conditions at snbient temperatures, the surface temperature of the package will vary from 98'F to 140*F for decay heat loads varying between j
300 and 1000 watts.
The contents of the packages are stable and will not be affected at these temperature conditions.
Even under exposure to 100*F and a solar load of 400 cal /cm2 the equilibrium temperatures will be less than 210*F and will not exceed values under which the contents of the packages would be affected.
J s
r i
2-9b Rev 2 - 4/1/86
(~)
1 1
1
A 2.~ 5 Hypothetical Thermal Accident Evaluation The THERMOS computer program and an analytical model was used to determine the temperature of key areas, such as the seals, the cavity bulk coolant and the general distribution for calculation o'f thermal stresses.
Maximum temperatures will occur when the cask is considered to have the full 0.30 KW internal heat generation,. full solar load and an ambient temperature of loo *F.
This starting condition was simulated by assuming an initial uniform temperature of 150*F for the transient analysis.
2.5.1 Analytical Thermal Model The maximum pressure in the cavity will be determined by the average temperature in the cavity.
To be conservative and calculate a higher than average temperature in the cavity, it was assumed that the inside surface of the inner shell was adiabatic.
This resulted in an upper limit on the cavity temperature and eliminated the need to model the contents.
{)
There were two analytical models used: the closure region and the central section.
Drain seal temperatures were deduced from these two analysis.
Each model was assumed to be axisym-metric.
The lead was assumed to be in perfect contact with the shells.
It was also assumed that the gap between the fire shield and outer shell was a mixture of air and stainless steel except where the fire shield attaches to che closure ring.
This was a solid connection.
There is a radial air gap between the cask and the aluminum impact limiter can, a layer of asbestos around the can, and a contact con-ductance of 1000 Btu /hr - ft2 _ er between the can and the top portion of the closure lid.
()
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2-10 ANEFCO, INC.
1 3
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After the fire, the cask is cooled naturally in 130*F ambient air.
The cask surface emis-sivities after the fire were conservatively assumed to be the same as before the fire.
Both the decay heat load and solar heat load were ignored during and after the fire.
Initial conditions before the fire were a uniform tem-perature of 150'F.
Closure Model The gap between the inner shell and the closure shield outer support ring was treated as a conductance of 11.5 Btu /hr - ft2 _ oF, the air spaces in the closure assembly were analyzed for radiant heat transfer and were then simu-t lated by a solid material.
See Figure 2.6-3.
Central Model See Figure 2.6-2.
Hand calculations were performed to compute the outside surface heat transfer coefficient
'()
between the fire shield and the environment, the asbestos and the environment, the effective conductivity of the aluminum can air gap, and the fire shield air gap. (See section 2.6.4) 2.5.2 Package Conditions and Environment Beginning with an assumed ambient temperature of 100*F, full solar and decay heat load, the cask experiences a 30-foot drop onto a flat surface followed by a puncture.
This is assumed to result in the complete and instantaneous loss of insulating crash barriers.
Concurrent with this loss, the cask is exposed to a thermal radiation environment of 1475'F for 30 minutes with an emissivity coefficient of 0.9 and a cask surface absorption coefficient of 0.8.
O 2-11 ANEFCO, INC.
t
A
~
"O Temperatures, Central Slice f
T = 1800 sec (end of heating) (with spacers)
)
Node Location Ternp *F Diameter-in.
2 Inner Shell Center 467 28.625 3
Lead 472 30.125 4
Lead 476 31.875 5
Lead 481 33.626 6
Lead 489 35.375 7
Outer Shell 511 36.850 8
Outer Shell 554 38.050 i
9 Outer Shell Surface 601 39.250
~
10 Fire Shield Surface 1108 39.875 l
4 I
I 1
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2-12 ANEFCO, INC.
.e i
LCS t
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t i
F 2.5.3 Package Tempera'tures A summary of the results is shown in Table 2.6-1
)
and Figure 2.6-4.
The thermal time response of i
selected points in the cask during and af ter the l
fire accident are shown in Figure 2.6-4.
The results may be summarized as follows:
I The maximum temperature in the closure seal i
a.
area is 473 F and this occurs just after i
0 completion of fire.
b.
The maximum lead temperature is 489 F, and f
0 this occurs at the central section just-after I
termination of the fire.
f i
i 2.5.4 Maximum Internal Pressure j
The cavit'y pressure is increased because of the l
rise in temperature.
Initially the air was loaded l
at.1000F and one atmosphere.
The final temperature l
,l,(])
was calculated to be less than 500 F.
This value 0
will raise the internal pressure to 25 psia, which is less severe than the design conditions of 115 i
0 j
psia at 600 F.
2.5.5 Maximum-Thermal Stresses j
.i l
2h'is condition will occur when the average tempera-
[
ture of the outer shell is most different from the l
average temperature of the inner shell.. This tempera-l ture difference produces a differential axial growth l
I.
and stresses the drain line.
This difference reaches a maximum of 76 F, about twenty minutes after start i
0 of the fire.
However,.this one time stress is'self limiting and there is no need for a fatigue analysis..
l i
2.5.6 ~ Evaluation j
The maximum temperature anc pressure-in tlle cavity
[
were< calculated to be below the design temperature
~
and pressure, so that the use of design conditions for the structural analysis was adequate.
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ANEPCO, INC.
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i Cyclic temperature differences produced by normal l
i
-operating conditions are lower than the design temperature differences so that these structural calculations were also conservative t
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l 2.6 APPENDIX 1
Equivalent Conductivity.of Air Gap 2.6.1 Description of THERMOS
{
2.6.2
- 0
^
Calculation of Steady Slate: Surface Heat Transfer 2.6.3 Coefficients I
Calculation of Transient Surface Heat Transfer 2.6.4 Coefficients I
THERMOS Input and Output-Data
- (
2.6.5 l
I i
l i
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I 2 ANEFCO, INC.
l
~. _
v i
c i ts 2.6.1 Equivalent Conductivity of Air Gap 4
It would be conservative to assume that the outer shell, spacers and fire shield remain in contact i
during the fire.
In reality, the fire shield will expand more than the inner shell due to the differ-ence in average temperature.
Therefore, the assumption i
of continuous contact will tend to produce higher predicted temperatures.
l 1
l
'K = h A = 6. 6 6 +.12 5 = 0. 07 Btu /hr-ft - 'F i
12 J
Effect of spacers
{
Total volume ratio I
.0196 2
TT x (0.125)2
= TTd
=
=
4dL 4
.125 x.5 l
r effective k I
i k =.0196 x 9 =.176 L
Total effective conductivity = 0.246 Btu /hr - ft *F 4
r i
i
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2-17 ANEFCO INC.
2.6.2 Description of THERMOS I,
S%
v THERMOS p: )
The Dynatech General Thermal Program is used to determine thermal i
i transients and steady state temperature distributions.
The program utilizes
{
~
an explicit finite difference technique. The modes of heat transfer can be i
either conduction or convection.
i The program can be applied to an arbitrary two dimensional geometry.
i A node is defined as a mass point representing a zone, which has a finite ther-j mal inertia and conductance to the neighboring nodes.
The temperature at each node is calculated during an iteration using the temperature distribution from the previous iteration.
L l
A maximum of 1600 temperature points can be determined using up to i
9 different materials and 10 different boundary conditions.
Special program-t ming is done to account for the effects of bolts in a closure analysis.
i
>N The program is run in two phases. Phase 1 is a preprocessor which converts the input geometric description into a form suitable for direct solution.
Phase 2 is the main program which calculates temperature distributions at selected I
values of time.
Phase 1 - Output The phase 1 output variables and constants are defined in the fol-loving section. Becaase of the options in the program,not all output will be k
present in a particular run.
This applies to both the phase 1 and phase 2 I
output.
i t
The basic input unit is a cell surrounding a modal point.
O i
2-18 1'5'
k
[
- T Surface 1 yX b)
I i
Mat'l Mat'l h*
Y
[
a I
b o
o Surface Mat'l Mat'l h
l R
x 1
c i
d Y
ti l
,1 i
r i
l l
l Y
l h
h j
Y Il o
4 o+M-1->
Node Dia.
Surface 3 Output consists of 1.1)
Mesh Si:c :nd Titic r
1.2)
Description,of Cells - Interior Data
^
O a)
Category number.
i
.i b)
Column number of node points.
c)
Two numbers defining the first and last numbers of con-secutive rows in column a).
d)
Node circle diameter (all columns, rows and diameters must be in increasing order).
f e)
X0, X1, YO, Y1 - See figure.
f)
HX0, HX1, HYO, HY1 - Film coefficients on surfaces 2 and
[
3.
A zero value indicates that there is no additional f
resistance between the node and the adjacent node, g)
Material Code - Indicates the set of material properties to be used:
e.g.
1122; for nodal sections a; b use the property set for material 1 (defined in 1.4) and for nodal sections e, d use the property set for material 2.
A single number means use that property set for a, b, c and d.
IO 2-19
- 2. 4.1.- L
t
/.w.m f
s-i lI h h)
Variable h code - Specifies which of variable h curves I
(phase 2) is applicable to surfaces 1, 2, 3, and 4 in l
T 1
order.
l I
1)
Special - Inoperative.
I 1.3) Boundary Data - Describes the surf ace conditions at boundaries l
of geometry described in the interior data (1.2).
All nodes
{
1 adjacent to the geometry must have conditions described, j
^
i I
i a) Columns - Column numbers of node points at which film f
coefficients apply, I
[
b)
Rows - Row numbers of node points at which film coefficients i
apply.
c)
HX, HY - Film coefficients'between the boundary nodes and
[
- (..
the adjacent interior nodes to the right (HX) and below i
(HY) the boundary (Cell surfaces 1 and 4).
U T
d) Potential Function - Indicates which temperature function applies to the surface.
1.4) Material Data l
a)
Code - Material identifier (See 1.2 -g).
i i
b) K and RHO-CP - Material conductivity and the product of l
i i
density and specific heat.
i c) Description - Material name.
\\
1.5) Table of Conductivities - (Output from Phase 1) a)
Column and row number of cell or cells.
i i.
i,
)
b). Cell numbers.
i 2-20
.'. 6.1-3
' riS i
- hh-D U
7 c)
C1, C2, C3, C4 - Conductivity between node point and adjacent nodes.
O i
I 3
s 0-C C
-0 2
4 1
1 0
d)
RHO-CP-V - Product of density, specific heat, and volume for the cell.
e) Max-T-Sec - Maximum allowable integration time step for this cell.
j f) Variable H Code - See 1.2 -h).
1.6)
Boundary Temperature Function Specification (Output from Phase 1) i a)
BEGIN-I, END-I - Cell numbers.
b) 3TEP - Number of cells, c) TEMP-FUNC - Temperature potential function (1.3 -d).
1.7) Maximum allowable integration step for this model and the total number of cells. An estimate of the solution time for a single step is also presented.
Phase 2 Output Phase 2 output consists of a printout of temperature functions and other input information along with the node point temperatures.
l) -
2.1)
Time increment used, initial temperature, print time increment V
and maximum step time for the integration.
2-21
- 2. $.1 'f
- /*
, Q.S.
+r l,_-)
2.2)
Option Controls IQ
= Initial Ten;. Code:
1 = uniform 0 = non-uniform IQ1
= Non-Uniform Initial Code:
+1 = Read from L4 0 = Read from L3
-1 = Read from cards I BOLTS
= BOLTS Subroutine Code:
1 = with BOLTS 0 = without BOLTS N B0'LTS
= Number of bolt nodes j
LA HEAT
= Latent Heat Subroutine Code: 1 = Call INLATE 4
0 = Bypass INLATE
()
J HEAT
= Latent Heat Printout Code:
+1 = Array with each Printout 0 = No Latent Heat Printout
-1 = Array on last Printout only I SEAL
= SEAL Subroutine Code:
1 = with Seal interpolation 0 = without Seal interpolation l
I SET
= Number of nodes with Periodicity INTERN
= Number of nodes with internal heat generation NQ1
= Number of internal heat generation curves NTQ1
= Number of times q curvea are specified IVH
= Variable H Code: +n = with variable H, n = No. of H curves 0 = without variable H NT
= Number of times H curves are specified 2-22 2.6 1."~
~?
ceU
- { i IDT
= Number of times time step (DT) is varied NPT
= Number of times print interval is specified l
NTEi' O Write out intermediate conductance in variable h option.
l INPACC
=1 Fixed point output for Seal interpolation 0 Floating point output for Seal interpolation NSTE
=1 Extrapolate to steady state
[
=0 No i
1 2.3)
(Optional) Variable Print Time Information VARIABLE PRINT TIME INCREMENT AT TIME (Times at which new print interval starts)
PRINT TIMI INCREMENT (Times between printouts) i O
2.4)
Boundary Temperature Information POTENTIAL FUNCTION NO.
(Number corresponding to 1.2)
TIME (times at which temperature is defined)
TEMPERATURE (Temperature values, 'F; linear interpolation)
- 2. 5)
(Optional) Five Temperature Interpolation Information (Seal) a)
BOUNDARY HEAT IRANSFER COEFFICIENTS (Values used in interpolation) b)
SEAL INTERPOLATION DATA COLUMN DIAMETERS (No. of columns; values of diameter)
'O_
2-23 g g,7_4
~
If7S l
g',
ROW ELEVATIONS (No. of rows; values of elevation, positive do.n) c) Description of individual interpola: ion geometry, columns first, rows from first negative (Serial number; a
column or row number; type of left-hand boundary; type of right-hand boundary; positica of: left-hand temperature, right-hand temperature, left-hand boundary, right-hand boundar);
thermal conductivity) 2.6)
(Optional) Periodicity j
l THE FOLLOWING (Number) NODES RETURN TO ORIGINAL TEMPERATURE AFTER EVERY (Value)
SECONDS (Node numbers corresponding to 1.5 -b) l QUASI STEADY STATE IS REACHED IF THE TEMPERATURE CHANGE BETWEEN TWO PERIODS IS l
LESS THAN (Value) 2.7)
(Optional) Internal Heat Generation j
- a)
THE FOLLOWING (Number) NODES HAVE INTERNAL HEAT GENERATION N0DE NUMBER (Node numbers corresponding to 1. 5 -b)
?
HEAT GENERATION CURVE NUMBER (Number of heat generation curve defined in 2.8 -b applying to node above) l b) CURVE NO. (Number)
TIME (Values of time increasing value, seconds)
I (Heat generation rate, degrees per second) 2.8)
(Optional) Input Data for Variable Heat Transfer Coefficient i
HEAT TRANSFER AREAS (Values of areas for surfaces 1, 2, 3, 4 in order for each
'{~}
category in order) 2-24
- 2. h,1 -)
i
- O
. v-4V (Numbers corresponding to variable heat transfer coefficient curve for surfaces 1, 2, 3, 4 in order for each category in order, categories from 1.5 -b) t 2.9)
Cells a) NO OF CAT - Number of categories i
b) IBC
- Number of boundary conditions c) MAXDT
- Maximum allowable integration time step
{
[
f d)
X, Y
- Mesh size i
e)
IZZ
- If IZZ = -1 the phase 1 output is in error, 2.10)
Conductances t
Output is by category number. The cell l
numbers are in the phase 1 output, 1.5 -b).
l i
2.11) Variable Heat Transfer Coefficient Curves as a Function of Time
,t or Node Temperature a) THERE ARE (Number H CURVES AS A FUNCTION OF TIME TIME IS (Values of time or temperature)
CURVE NO.
(Number, Values of heat transfer coefficient, f
linear interpolation) b)
(Values of heat transfer resistance without surface coefficient for all surfaces 1, 2, 3, 4 for all node categories) 2.12)
(Optional) Variable Time Step Interval i
VARIABLE TIME INCREMENT AT TIME (Values of time) i TIME INCREMENT (Values of time step) 2-25 2I.2-8
dbg V
P w~s 2.13) Temperature Output
.V.!
Time of output, time increment and printout number along with the temperatures at each node point.
The output is in I
matrix format. Non-active cells are printed as zero. The
{
output should be interpreted with reference to the model i
drawing.
Boundaries temperatures are printed at node points adjacent to the interior geometry.
2.14)
(Optional) Bolt Temperatures BOLT TEMPERATURES - B1, B2,... B(Number)
(Values of temperature at specified bolt node) 2.15) (Optional) Latent Heat Distribution i
THE LATENT HEAT ARRAY IN DEGREES FOR THE PREVIOUS ITERATION IS l
( )
(Array by rows and columns of residual values of latent heat for nodes which are 1
melting or solidifying) 2 16)
(Optional) Seal Temperature Interpolation (Series number, column or row, values of temperatures at five equally spaced points whose positions are defined in 2.6) i i
i r
f f
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[
t 2-26 2.f,2.-T
...^.
O i
2.6.3 Calculation of Steady State Surface Heat Transfer Coefficients i
One dimensional model j
I 1.
Outside Surface - Steady State i
h
+h l
h
=
C r
j h
=.21 (6T)1/3
- 0.21(50) 1!
= 0.77 Btu /hr-ft F c
i j
h 4(7Tm M (4.) (0.1715) (. 25) (130+4 60) 3 l
3 r
108 j
i I
\\
I h=4=0.25=.35 Btu /hr-ft F f
I i
O Stainless steel at room temperature, no fire l
l blackening h = 1.12 i
l i
l k
^^
I i
l E
-i l
i I
O 2-27 ANEFCO, INC.
l
r w-0 2.6.4 Calculation of Transient Surface Heat Transfer Coefficients Assume T shield
- 1475 F (1935 R)
Air gap 400 F (860 R)
T cask
[=1/[(1/g) + (1/E) -1] = 1/[(1/.52) + (1/.6)-1]
f=0.39 h
=[ (T1+T) (T1 +T2) 2 r
-8 2
= 0.1715 x 10 (0.39) (860 + 1660) (8602 + 1660 )
h
= 5.89 Btu /hr OF ft
~
r (021/2) (4 T/2)1/3 h
0.105 (400)1/3
=
=
c i
h 0 77 Btu /hr-ft - F
=
c 6.66 Btu /hr-ft - F h
=
I r
O 2-28 ANEFCO, INC.
,e u.x U
Calculation of Heat Transfer Coefficients Calculate the thermal response to a fire atmosphere at 1475 F for thirty minutes, followed by three hours without artificial cooling.
Emissivity during heating 0.9 with surface emissivity 0.8.
Assume an atmosphere of 100 F with an absorptivity of 1 during cooling.
0 T = 1475 F (1935 R)
- h = Jc- (T 2+T
- 2) (T1 + T) + h conv 2
- PrGr = g (T
- Too 2L (facp/k) o O
s = P/RT = (14. 7) (14 4 ) /53. 3T B=
1 T
(1935-T)!14.7x144
/(.1+200 2
3 PrGr = 32.2 x (3600 ) 3 1+340' d
T T
53.3 I
(002264x/00109 1
'I Rowsenow & Chu, Heat, Mass Momentum Transfer, John Wiley, 1962, p.346 O
Pese 204 2-29 AN EFCO, INC.
t
,e
~
1 s
'O Viscosity and Thermal Conductivity Equations
.013 (GrPr)1! '
hD/k
=
.00109 8 h
=
1 + 340 T
32.2 x 3600 (1935 -T) 14.7 x 144 X
1+ 200 (1.+ 240 1/3 2
T T
T4 53.3 l
(.00264 x.00109 /
l 8
2 h1= [0.00109 /T / (1+340/T] (179,~250/T ) [ (19 35-T) (T+200)
(T+340) ]1/3 f
i h1 = 195.4/ 6 [(1935-T) (T+200) / (T+34 0) 2 ) 1/3 O
i
.sg
}
I
{
t i
+
Kowsenow & Chu, Heat, Mass Momentum Transfer, r
John Wiley, 1962, p. 205 j
2-30
,u,,ca,,ue,
i
?
Use Sutherland formula for properties L/
Thermal C
Viscosity Conductivity p
R lbm/hr-ft Btu /hr-ft UR Btu /lb OR r
560
.046
.016
.241 1960
.106
.041
.277 1
(T) 3/2 / (T + C )
- ** P = Cy 8/(1+C /T) =C1 2
2 (T /T )
(T
+C) / (T
+C)
(Py/P )
=
2 y
2 I
i (T
P /P ) + (C P /P )
=T (T /T )
+C (T /T )
2 2
y 2
2 y
2 2
y 2
O 3/2 3/2
= -T (T /T )
+T (P /P )
(P /P C
(T /T )
y 2
1 y
2 y
2 T
(1/T )
-T (P /P )
2 y
y 2
C2=
2
-(T /T )
+ (P /P2) y 2
y Thermal l
Viscosity Conductivity i
200 340 C2 Cl
.00264
.00109 6
A V
Page 498 and Page 500 l
2-31 ANEFCO, INC.
^
y J = 1/ [ (1/E) + (1/E )-1] = 1/ [ (1/. 9)
(1/.8)-1] = 0.735 2
HEATING Econd 2
F R
hrad Btu /hr-ft F Total i
O t
100 560 12.76 8.99 21.75 300 760 14.68 6.92~
21.60 t
500 960 17.02 5.52 22.54 800 1260 21.46 4~.00 25.46 l
1000 1460 25.14 3.9 28.33 1200 1660 29.44 2.42 31.86 I
- Q 1475 1935 36.52 0
,36.52 i
t COOLING 100 560 0.89 0
2.9 120 580 0.93 2.14 3.07 200 660 1.15 3.36 4.51 300 760 1.48 3.84' 5.32 500 960 2.37 4.10 6.47 800 1260 4.36 4.05 8.41 l
1000 1460 6.22 3.96 10.17 i
1200 1660 8.59 3.84 12.43 1475 1935 12.76 3.68 16.44 i
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Page 347
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HEAN XO XI YO Y1 HX0 HXI
- HYO'~~ HY1 MATL' VAR H' SP EC I AL~~ ~~ ~
INTERIOR DATA CODE CODE CATEGORY FROM TO DIA
-0 01 6
10 10 29.250 6250 2310 2.0000 2.0000
-0
-0
-0
-0
~~1313' 42 6
11 11 29.250 6250 2310 3.1880 3.1870
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-0 1***
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7 2
2 31.270 _. 7790 2310 1250 2500
-0
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31.270 7790 2310 1.2500 1.2500
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45 7
4 4
31.270 7790 2310 2310 7690
-0
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-0
-0 1
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7 5
5 31.270 7790 2310 1.2500 1.2500
-0
-0
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---O'~--"---'
47 7
6 6
31.270 7790 2310 1.3750 1.3750
-0
-0
-0 48 7
7 7
31.270 7790
.2310 1.7500 5000
-0
-0
-0
-0 3
-0
-0
-0 3
-0
__. 4 9,__ _ _ 7
_. 8 8_.
31.270._
7790
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-0
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~~-0 50 7
9 9
31.270 7790
.2310 ~
8750
.8750
-0
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$1 7
10 10 31.270 7790 2310 2.0000 2.0000
-0
-0
-0
-0 3
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__.52 7
_ 11.11 31.?to 7790
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-0
-0
~-0 3
-0 53 8
2 2
33.992 1 1300 1.1290
.1250
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-0
-0 ~ ~ -0 ~~5544 -'1***-~~~-0~~
54 8
3 3
33.992 1 1300 1 1290 1 2500 1 2500
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4 33.992 1.1300 1 1290
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33.992 1.1300 1.1290 8750
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2 2
37.750 7500 7500 1250
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o 65 9
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37.750 7500 7500 2310 7690
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6 37.750 7500 7500 1.3750 1.3750
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68 9
7 7
37.750
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69 9
8 8
37.750 7500 7500 1.5000 1.5000
-0
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0
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__ 7 0 __ _. 9 9
9 37.750
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- ' - ~ '0 71 9
10 10 37.750 7500 7500 2.0000 2.0000 72 9
11 11 37.750 7500 7500 3.1880 3.1870
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__ 73 __
10 2
2 39.500
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-0 8121
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10 5
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-0 2121
~-0 _
77 10 6
6 39.500
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-0 2121 O
78 10 7
7 39.600
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8 39.500 _.1250
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INTERIOR DATA l
_ INPUT _.. _.. _
POWS MEAN.. XO X1 YO Y1 HX0
~ HX1 HYO HY1-- M ATL'--~~V AR H'~~5PECI AL:
COL.
CODE CODE
- j ()
CATEGORY FROM TO DIA
- t 81 10 10 10 39.500 1250
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-0
-0 2121
+ 1 * * ~ ~ ~~ - O ~ -~
!O 82 10 11 11 39.500 1250
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__ 83 11 2
2 40.500 2500
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e 84 11 3
3 40.500 2500
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()
85 11 4
4 40.500 2500
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5 40.500
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6 40.500 2500
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FROM TO FROM TO
. FUNCTION 0
35 1
~ -
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1 1
2 11 0
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12 12 2
6 1
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MATERIAL DAT.A _. DESCRIPTION.
CODE K
RHO-CP 1
11.000 54.00 STAINLESS STEEL.
2 246 1.08 AIR GAP WITH SPACFRS' ~
3 63.000 41.00 LEAD
._e_.-
4 119.000 36.20
. _ ALUMINUM S
130 9.00 ASBESTOS 6
104 -
.14 AIR GAP AT TOP AIR SPACE 7
2.850
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~
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9 000
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_ TIME INCREMENTn 1.00000_
INITIAL TEMPERATURE =
150.000 RHINT TIME INCREMENT =30:n00000 MAXIMUM TIME = 1800.000 O'
- - ~ ~ - - " - ~ - - - - -
iqs 1
10l=
-0 IROLTb=
-0 t: BOLT S=
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8
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INPACC=
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POTENTIAL FUNCTION DATA
!O s
.ROTENTIAL FUNCTION NO.
1 TIME
.0 1800 0
,O TEMP 1475.0 1475 0
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_CINDUCTANCES HOTTON
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()
56 550396 48.612310 12.871u18 7.In5983 5 969026 94J73216 63.325797
.000000 62 609350 53 820758
- j
_. 17.698483 10.942436 9.191646 104.617462 70.110131 000000 156.73H180 134.736547 35.674021 19.695333 16.544080 261.902584 175.515668
.000000 167.457177 143.950H98 64.213772 44.316706 37.226033 212 814732
- - " - ~ -
'-j ()
149.706728
.000000 55.873456 48.o30394 35.231804 32.788684 52.429735 81.921462 68.986494 56.988843 t
_ 31.581134
.000000 70.188d87 60.136083 44.258414 59.968442 163.768365 255.888070 215.484690 178 009092
'g 98.646133
.000000 173.690399 149.109151 109.522958 14A.399379 405.265213 633.226895 533.243701 440 505666 CD, 244.112142
.000000 128.086646 110.106883 H0.766862 62.121255 52.181854 81.534147 68.660334 56.719406
' j
__ 31.431822
.000000 323606 322940 14.331316 11.022829 9.259177 14.467464 12.183127 10 064323 5.577280
.000000 209.107488 211.790164 155.354746 119.489993 228.117260 4
f%
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_ CONDUCTANCES LEFT 00u000
.000000
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.000000 000000
.000000
.000000
.000000 27 199951 25 129086
~ ~ " - -
5 10 051634 7.189330 7.908263 10 058348 172 705355 8.795260 29.878521 27.603724 11 041489 7 151874 7.867061 10 527056 189.712864 9.661'91 45.464093 42.002690 16.801076 10.H82515 11 970767 16 018299
.. 288.673032 14.701075 129.264223 119.422706 6 124306 15.310765 16.841842 13.779689 18.372918 5 359371 I^
000000
.000C00 229.246790 211.793112 84 717245 211.793112 1334.296608 1091.697225 1455 596300 849 097842
.1940 795066 3093 142137 161 690438 167.657457 67 142983 167.857457 1057.501982 865.228894 1153 638525 672 955806 i
1538 184700 2451.481866 150.339805 138.893701 55.557480 138.893701 303.105492 247.995403 330 660537 192 885313 - - - - ~ ~ ~
5 440 880716 702 653641 349.562116 20.225940 40 324813 44.574934 49.032427 40.!!7441 53 489921 31 202454 s
__ 71 319894 113.666082 214.900443 10.R81345 9.802409 24.504021 26.956623 - -
CONDUCTANCES TOP 94.493216 63.325297 5 555240 62 609350 5 017638 56.550396 46.612310 12.871018 7 105983 5.909026 1
_. 53.820758 17.698483 10 942436 9.191646 104.617462 70 110131 13.907160 156.738100 ~134.736547 35 674021 j
19.695333 16.544080 261 902584 175.StS868 14.858242 167.457177 143.950898 64.213772 44 316706 37 226033
_ 212 814732 149.708728 4.957574 55.ai3456 48 030394 35.231804 32 788684 52 429735 81 921462 68 986494 i
56.988843 31 581134 6 227735 70.188587 60 336083 44.25H414 59.968442 163.768365 255 888070 215 484690 ~- - - " - - -
s j
178 009092 9R.646133 15.411307 173.490399 149 309151 109.522958 148.399379 405.265213 633 226895 533 243701 l
__440 505666 244 112142 11 364950 128 0 6646 110 106883 80 766862 62 121255 52 181854 61 534147 68 660334 8
4 56 719406 3i.431822 2.982358
.323606
.322940 14.331316 11 022829 9.259177 14.467464 12 183127
[f ~~~
10 064323 5.577280 3 038807 209.107488 211 790164 155 354746 119.489993 a
(N
-CONDUCTANCE 5 RIGHT 27 199951 25 129c86 10 051634 7 189330 7.908263 10 058348 172.705355 8.795260 29 878521 27 603724
__ !!.041489 7.151874 7.A67u61 10.527056 189.712864 9.661391 45.464093 42.002690 16 801076 10 882515 a
11 970767 16 018299 288.673932 14.701075 129 264223 119.422706 6.124306 15.310765 16 841042 13 779689 -
~ ~ - ~
18 372918 5.359371 229.246790 211.793112 84.717245 211.793112 1334.296608 1091.697225 1455.596300 849 097842
)
_1940.795066 3093 142137 181 690438 167.957457 67 142983 167.857457 1057.501982 865.228H94 1153 638525 672 955806
-~
1538 184700 2451 4H1866 150 339005 138.a93701 55.557480 138.893701 303.105492 247.995403 330 660537 '192 885313 440 880716 702 653641 349.562116 20.225940 40 324813 44.574934 49.032427 40 117441 53 489921 31 202454 71 319894 113.6660H2 214.900443 10.981345 9.802409 24.506021 26.956623 64.450080 85 933440 50 127840 i
i
__ 114 577920 182.60H560 3.06703) 20.446874 8 178750 20 446874 22,491561
' -~ ~ - - -
. RHO-CP-V
.462467 6.135923 2.454369 015908 017499 1 238320 5.590508~
2 147573 ~~
.512017 6 793342 2 717337 943748 1.038123 2.019292 6 189489 2.377670 1.281798 17.006661 6 802665 044091 1
.046500 3.432196 15.494958 5.952331 1 369458 1H.169711 7.267A85 7.056735 7 762408 8 573657
_ _. 18.584893 6.359399 456931 6.062473 2.424969 6.062473 6.226095 -~ 5.094077
~ 6.792103 3 962060 ~ ~ ~ - - - - - - - -
9.056138 14.433219 573999 7.615716 3.046287 7.615716 6.360533 5.204073 6.938764 4 047612 9.251685 14.744873 1.420433 18.A46039 7.538415 18.846039 15.739932 12.878126 17.170835 10 016320
]
~~~ 22.894447 36.488025 1.047487 13.897866 5.559146 13.897866 15.287653 12.508079~ 16.677439 - 9.728506 1
22 236585 35.439558 274879
.009455 1.043401 2.463190 2.709509 2.216871 2.955828 1 724233
__ 3.941103 6.281134 217302 1.H63346
.745339 1.853346 2.049681
~THERE ARE
-1 H CURVES AS FUNCTION Or TIME
~
~~ ~~ ~~~
TIME
.000 100.u00 300.000 500.000
.aD0.000 1000.000 1200.000 1475.000
.000
.000 con i
Ts,ang 71.7so 23.6n0 -
72.560
. 460 78.330 3 3. a c,o 36.520
.000
.000
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7-4.
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.t
~-4 7
)
NUCLEAR CASK CORNER COVER HEATUP AFTER 300 00000 SECONDS, 300 RUNS, TIME INCREMENT 1 00000 SECONDS, PRINTOUT NO.
1 I:
f.
3 0 1475 1475 1475 1475 1475 1475 1475 1475 1475 1475 0
0 287 287 288 294 304 314 336 408 474 573 1475
~
0 201 201.201 202 206 259 216 240 383 653 1475 3
0 175 174 175 173 172 174 178 196 273 695 1475 0
166 160 165 155 154 155 157 170 312 754 1475 ~
' '- ~ ~
)
L _ __. 0. 1 5 6 153 156 151 168 159 161 174 379 855 1475 3
0 150 150 150 150 163 165 171 219 818 1475 0
~
~ ~ ~ ~ ~ ~ ~ ~ ~ - ~
0 150 150 150 150 166 168 174 227' 860 1475 0
--. 0 150 150 150 150 167. 170 176 228 864 1475 _ 0 3
0 0
0 0
-0 16is 170 176 229 864~1475 0
0 0
0 O
O 168 170 '177 229 864 1475 0'
'-~~
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6 3.
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~
NUCLEAR CASK CORNER COVER HEATUP AFTER 600.00000 SECONDS, 600 RUNS, TIME INCREMENT 1.00000..SEg0NDS, PRINTOUJ NO.
2 O 1475 1475 1475 1475 1475 1475 1475 1475 1475 1475 0
0 330 331 334 345 363 377 407 494 568 677 1475 6
._..__._0 247.247 248 252 262 271 287 327 481 770 1475 0
'216 214 216 212 214 219 231 268 373 822 1475 0
197 187 194 174 177 180 188 219 426 894 1475 6
____.___.0
.172 166 170 159 190 193 197 222 503 1007 1475 O
152 152 152 194 203 206 214 277 897 1475 0
0 151 151 '.151 153 210 214 222 292 940 1475 0
~
4
_.._._0.
150 151 151
.193 215. 219 227 296 946.1475 0
0 0
0 0
0 219 223 231 299 948 1475 0
0 0
0 0
0 221 224 233 300 948 1475 0
__._0 0
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0 0_ _ 0.._ 0 0
0.. __ _0. _.._ 0. _ __
7
._ _ L.
'^'
9 0
~
~~
~~
~~
NUCLEAR CASK CORNER COVER HEATUP O-AFTER.
900.00000 SECONDS, 900 RUNS, TIME INCREMENT 1.00000 SECONOS, PRINTOUT NO.
8
(
D 0 1475 1475 1475 1475 1475 1475 1475 1475 1475 1475 0
0 371 372 376 392 414 431 465 554 626 735 1475 0
--0 289 289 292 300 315 327 349 395 545 827 1475 O
O 257 254 258 253 262 269 286 332 440 880 1475 0
229 219 227 202 215 221 233 273 492 954 1475
~
_ _. 0 191 183 189 175. 234 237 242 271 566 1070 1475__
O O
155 155 156 161 249 253 262 325 930 1475 0
~
~ ~ ~ ~ ~ ~ '
~ ~
~ ~ ~ ~ ~ - - - -
0 153 153 155 158 259' 263 272 342 970 1475 0
.., _ __ 0 152. 152 154 158 267 271.280 350 978 1475
_. 0 O
0 0'
0 0
0 275 278 287 355 981 1475 0
0 0
0 0
0 280 283 291 358 982 1475 0
4
.. __ _ 0 0
0 0
0 0
0 0
0 0
0 0
O t
Q...
. -.-..Q
NUCLEAR CASK CORNER COVER HEATUP AFTER.
1200.00000 SECONDS, 1200 RUNS, TIME INCREMENT 1.00000 SECONOS, PRIN70VT'NO.
4 b.
- s
- [
s 0
0 1475 1475 1475 1475 1475 1475 1475 1475 1475 1475 D
0 409 410 416 435 460 479 514 603 673 778 1475
_ ___. _ 0 329. 330 334 345 365.. 379 404 452 597 868 1475 0 '296 294 299 294 311 320 340 388 494 920 1475 0
262 251 ~ 261 234 261 267 282 325 543 994 1475 g
._. _ 0 210 203 210 197 280 284 290 319 613 1111 1475 O
159 160 163 172 296 300 309 371 957 1475 0
0 157 158 161 167 306 311 320 389 995 1475 0
4
._._0 155 156 159 166 317 321 330 398 1003 1475 0
0 0
0 0
0 328 33'2 340 407 1007 1475 0
O 0
0 0
0 336 339 347 412 1010 1475 0
"~~
s
_.0 0
0 0
0 0
0
_. 0 0
0._.
0 0
O
NUCLEAR CASK CORNER COVER HEATUP i-AFTER 1500.00000 SECONDS, 1500 RUNS, TIME INCREMENT 1.,0 0 0_0 0 _ S E C O N D_S,
PRINTOUT NO.
5
(
,7 0 1475 1475 1475 1475 1475 1475 1475 1475 1475 1475 0
b 0.445 447 455 477 503 524 559 646 714 815 1475 6
-..0 368 368 375 389 411 428 454 501 641 902 1475 O
334 332 338 336 359 369 390 438 542 954 1475 0
293 283 294 270 308 315 330 374 588 1026 1475 9
_ _.._ 0 231 224 233 223 326 330 337 366 655 1144 1475 D
0 166 168 172 186 342 347 355 416 981 1475 0
0 163 165 169 177 353 358 367 433 1018 1475 0
m
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.--_ 0 161 162 166 177 366 370 379. 444 1027 147.5 _. 0 0
0 0
0 0
379 382 390 455 1032 1475 0
e 0
0 0
0 0
389 392 400 463 1036 1475 0
^..
3
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- Q.._.-
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NUCLEAR CASK CORNER COVEH HEATUP AFTER... 1800.00000 SECONDS, 1800 RUNS.. TIME INCREMENT 1.00000 SECONDS, PRINTGUT NO.
6
't L
0 1475 1475 1475 1475 1475 1475 1475 1475 1475 1475 0
0 479 482 491 516 544 565 601 685 751 849 1475
{
-404-406 413 430. 456'-
473 500 547 681 933.1475
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0 370 368 377 376 --405 415 437 485 585 984 1475 0
324 315 328 306 354 362 378 422 630 1056 1475
- - - - - ~ - _
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__ y, _0 252 246 257. 251 372 376 382. 411 694 1173 1475
/
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0 175 178 183 202 387 392 401 459 1005 1475 0
0 171 174 180 190 398 403 412 476 1040 1475 0
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.......0 168 171 176 190 412 416 425 488 1049 1475 0
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0 0'
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0 0
0 0
0 439 442 450 510 1060 1475 0
3
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0
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0 0
3
_ EXIT PHASE 2.
D g
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=
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.M6 a9".4=e am-un.>
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1 I3 id CONDUCTANCE 5 BOTTOM
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/>
56 550396 48.612310 12 871018 7.105983 5.969026 94.493216 63.325297 000000 62 609350 53 820758
_. 17.698483 10.942436 9.191646 104.617462 70 110131 000000 156.738180 134.736547 35.674021 19 695333
/
16.544080 261.902564 175.515d68
.000000 167.457177 143.950898 64.213772' ~44.316706 37.226033 - 212 814732 149.708728
.000003 55.873456 48.030394 35.231804 32.788684 52.429735 81.921462 68.986494 56.988843
? f
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ih
__ 31.581134
.000000 70.18Hd87 60.136083 44.25H414 59.968442 163.768365 255.888070 215.484690 178 009092 98.646133
.000000 173.690399 149.309151 109.522958 148.399379 405.265213 633.226895 533.243701 4 4 0 5 0 5 6 6 6 ~ ~ ~~- ~~~- --- '
i f) 244 112142
.000000 128.086646 110.106H83 H0 766862 62.121255 52.181854 81.534147 68.660334 56.719406
-)
i
_. 31.431H22
.000000 323606 122940 14.331316 11.022829 9.259177 14.467464 12.183127 10 064323 ~ ~ - - ~ ~ - ~ ~
i 5.577280
.000000 209.107488 211.790164 155.354746 119.489993 228.117260
- ?
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_ CONDUCTANCE 5 LEFT 00U000
.000000
.000000
.000000 000000
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'27 199951 2 5 12 9 0 8 6 ~ ~~~ --- ---~~ ~
/>
10 051634 7.189330 7.908263 10.058348 172 705355 8.795260 29.878521 27.603724 11 041489 7 151874 7.867061 10.527056 189.712664 9.661391 45.464093 4?.002690 16.801076 10.882515 11.970767 16 018299 -~~
j
__ 288.673032 14.701075 129.264223 119.422706 6.124306 15.310765 16.841842 13.779689 18.372918 5 359371 f)
.000000 000000 229.246790 211.793112 84.717245 211.793112 1334.296608 1091.697225 1455.596300 849 097842
,l 3538 184700 2451.481866 150.339dO5 138.893701 55.557480 138.893701 303.105492 ~ 865.228894 1153.638525 6 1940.795066 3093.142137 181.690*38 167.857457 67.142983 167.857457 1057.501982 247.995403 330.660537^~192 885313 --
d C) 440.880716 702.653641 349.562116 20.225940 40.324813 44.574934 49.032427 40.117441 53.489921 31 202454 j
_ 71.319894 113.666082 214.900443 10.kH1345 9.802409 24.506021 26.956623 5 017638 56.550396 46.612310 12.H71018 7 105983 5.969026 94.493'16 63.325297 5 555240 62 609350
~ - - ~ ~ - "
C3 CONOUCTANCES Top
_. 53.82uT58 17.698483 10.942436 9.191646 104.617462 70.110131 13.907160 156.738180 134.736S47 ' 35 674021 l
C) 19.695333 16.544080 261.902584 175.%I5868 14.858242 167.457177 143.950898 64.213772 44.316706 37 226033
_.212.814732 149.708728 4.957d74 55.873456 48.030394 35.231804 32.788684 52.429735 81.921462 68.986494 3
56.988843 31.581134 6.227735 70.188587 60 336083 44.258414 59.96H442 163.768365 255.888070 215 484690
()
178 009092 96.646133 15.411307 173.690399 149.309151 109.522958 148.399379 405.265213 633.226895 533 243701
_ 440.505666 R44.112142 11.364950 128.086646 110 106883 80.766862 62.121255 52.181854 81.534147 68.660334 a
56.719406 31.431H22 2.982358
.323606
.322940 14.331316 11.022829 9.259177 14.467464 12 183127 ~ - -- -
m-C) 10 064323 5.577280 3.038607 209.107488 211.790164 155.354746 119.489993
]f
- _ - _fi l
' CONDUCTANCE 5 HIGHT
. C) 27 199951 25.1290H6 10 051634 7.189330 7.908263 10 058348 172.705355 8.795260 29.878521 27 603724
_. 11 041489 7 151874 7.H67J61 10.527056 189 712864 9.661391 45.464093 42.002690 16.801076 10 882515
- - ~ ~ ~ ~ ~ ~
11 970767 16 018299 ?88.673W32 14.701075 129 264223 !!9.422706 6.124306 15.310765 16.841842 13 779689' d
] f3 18 372918 5.359371 229.2*6790 211.793112 84.717245 211.793112 1334.296608 1091 697225 1455.596300 849 097842 m
j
.1940 795066 3093.142137 181 690438 167.857457 67 142983 267.857657 1057.501982 865.228894 1153 638525 672 955806 -
~
j 1538 184700 2451 481866 150.339805 138.893701 55 557480 138.893701 303.105492 247.995403 330 660537 192 885313 i 43 440 880716 702 653641 349.s62116 20.225940 40 324813 44.574934 49.032427 40.117441 53 489921 31 202454 85.933+40 50 127840
__ 71 3.19894.113 6660H2 214.900443 10.H81345 9.802409 24.506021 26.956623 - 64.450080 ~~
~
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114 577920 182 608560 3.067031 20.446874 8 178750 20 446874 22.491561 (3
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_ RHO-CP-V a
J 2 717337 943746 1.03H123 2.019292 6 189489 2 377670 1.281798 17.006661 6.802665 044091
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~~ 18.58489s 6.359399 456931 c.a62473 2 424989 6.062473 6.226095 '-~ 5.094077 ~ ~ 6.792103 - 3 962060 -
we 9.05613a 14.433219 573999 7.615716 3 046287 7.615716 6.360533 5.204073 6.938764 4 047612 g
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~~' ~ ~ ~ ~
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.000 100.000 300 000 500.000 0.000 1000.000 1200.000 1475.000
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'THER E
-1 H CURVES AS FUNCTION OF TIMF I
35.000 2.900 5 320 6.470 8.410 10.170 12 430 16.440
.000 000
,i
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NUCLEAR CASK CORNER COVER COOLDOWN
~
~
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PRJNTOUT NO.
2 AFTER 300.00000 SECONDS, 300 RUNS, TIME INCREMENT 1.00000 SECONDS, __ _ _,,.
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0 130 130 130 130 130 130 130 130 130 130 0
0 385 389 399 421 441 454 470 487 489 494 130
..0 392 394 404.422 447 461, 483 508 506 502 130 0
382 382 391 394 429 438 457 488 ^ 513 509 130 0
340 337 347 337 395 403 417 449 519 518 130
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268 265 277 279 410 413 3171 433 518 521 130 0
186 190 197 219 419 423 427 443 4S9 130 0
0 182 185 193 205 428 432 436 454 463 130 0
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NUCLEAR CASK CORNER COVER C00LD05N
...AFTER 600.00000 SECONDS, 600 RUNS, TIME INCREMENT 1.00000 SECONDS, PRINTOUT NO.
3 0
130 130 130 130 130 130 130 130 130 130 0
0 376 380
'M 610 423 431 438 437 430 419 130 0
383 386 396 414 434 445 457 466 446 410 130 0
377 379 389 397 432 439 450 462 458 407 130 0
341 '342 353 356 418 424 433 446 448 403 ~ 130
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0 197 202 210 275 427 430 432 431 388 130 0
0 194 198 206 220 432 435 437 436 386 130 0
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m O
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N N
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4 N
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4 N
O O
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lA M
N 9*
f*
4 CD o
o O
4 e4 M
M M
M N
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- \\d a
g l
i O
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i i
7 a
r
.n 6
6 s-j i
4 l
l l
i I
I I
i i
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n..
I NUCLEAR CASK CORNER COVER COOLDOWN
~ ~ ~
~~~ ~-
AFTER 1200.D,000.0 SECONDS, 1200 RUNS, TIME INCRENENT 1.00000 SECONDS, PRINTOUT NO.
5
{
0 130 130 130 130 130 130 130 130 130 130 0
0 364 368 37R 392 399 402 403 395 386 372 130 0- 370 374 384.400 412 417 421 419 399 361 130 0
366 369 381 392 421 424 427 426 413 356 130 0
339 342 355 370 424 427 429 429 406 349 130 287 290 305. 378 424 425 i42k 424 397 343 130
__.(,, 0 O
221 227 236 261 423 424 425 421 365 130 0
~
~218 223 232 245 '425 426 427 422 363 130-~
0
~ ~ ~ - ~
~ ~
"-~ ~~~ - - - ~ ~
0
... 0.
214 219 228 245 432 433 433 428 367 130__.
O Li 0
0 0
0 0
442 442 441 436 373 130 0
4 0
0 0
0 0
454 453 452 447 382 130 0
- " ~ ~ ~ ~ ' ~ ~ ~ ~ ~
~~~~ ~ ~ ~ ~ ~ ~ -
~~
0 0
0 0
0 0
0 0
0 0
0 0
~
me@
e.'
e.-
, eme s
us..'"
.e-m_m
.ums.p,Wp
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G
=
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.O aq=6 m
~.
e,e e _ w e my a.m -ma p q. 4
= **
O_-4 pe+
wen e
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mge OO"*"*W
- N
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=
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e
1 i
a
'A
'kY 3.0 Containment _
This chapter of the Safety Analysis report iden-tifies and discusses the package containment for i
both normal conditions of transport and the hypo-thetical accident conditions.
i 1
}
3.1 Containment Boundry j
~
I This section contains a description of tdue. elments that make up the containment boundary and the poten-tial places of problems.
t 3.1.1 Containment vessel i
The containment vessel is made up of the inner shell, l
cavity bottom plate, closure ring and closure lid, t
This vessel was designed as a free standing pressure j
vessel, in accordance with Section VIII of the ASME' B & PVC, with the design. conditions of 600*F and 100 psig.
I 3.1.2 Containment Penetrations
!j)
There are a. total of three penetrations of the pri-l mary containment boundary.
One is the closure' lid j
at the top of the vessel and the other two are,the drain lines.
The, key element in sealing of the containment vessel against potential leaks of the contants.
All the redundant elastomer seals used i
to seal each of the three penetrations.
The tem-perature operatin@ characteristecs of these seals are shown in figure 2.3.1.
The maximum temperature-i of the seals in the hypothetical fire test is 473'F
['
compared to a material rating of 600*F for periods l
1ess than 48 hours5.555556e-4 days <br />0.0133 hours <br />7.936508e-5 weeks <br />1.8264e-5 months <br />.
3.1.3 Seals and Welds i
i Etch redundant seal used in the three penetrations of I
the package containment is composed of material which l
is a high temperature flourocarbon rubber elastomer.
l The seal used to seal the closure lid to the cavity l
ring is fabricated by the injection moulding of two i
concentric rings of the elastomer to and through a j
j 0.120 stainless steel gasket which is specially made i
to completely cover the top of the cavity ring The seal is attached by. set screws to the underside of i
l the closure lid and is readily accessable for in-spection and replacement as required during use.
i s
j i
3-1 ANEI8CO. INC.
l r
,_.1,_..,...
_,,..... _ _, _, _. - ~.
.J
' (7:
V-+
Seals and Welds (con't)
(
)
s-This type of seal offers the advantage of high' i
loading (100 pounds per linear inch) on the sealing surface to insure leak tightness as compared to typical elastomer O ring loading of 20 to 40 pounds per linear inch.
l f
The two cavity drains are sealed by redundent radial l
0 rings mounted on a plug which is screwed directly into drain connection welded to the Cavity Bottom Plate.
All welds are full penetration, in accordance with the Cask Designers Guide by L B Stappert and the ASME Boiler & Pressure Vessel Code,Section VIII, Division #2.
f 3.1.4 Closure There is a single closure assembly which is held in place by 20 of 1 1/2
-12 UNF bolts.
An initial bolt torque of 1,250 ft./lb. is used on these bolts to provide seals for 100 psig internal pressure.
,()
3.2 Requirenents for Normal Conditions of Transport This section contains a summary description of the results from Chapter 1.0, structural analysis and Chapter 2-0, Thermal Evaluation, to demonstrate that the package containment meets the requirements of Appendix A, 10CFR71.
3.2.1 Release of Radioactive Material There will be no direct release of radioactive material from the containment vessel because the maximum normal operating pressure differential across the seals is 9.6 psi which is less than the design pressure of 100 psi.
3.2.2 Pressurization of Containment Vessel The only mixture of vapors and gases that can form in the containment vessel are air and water vapor.
There will be no explosion within the containment vessel and any increase in pressure vessel parts.
The pressure increase will be only due to tempera-ture increases of the containment vessel O
3-2 ANEPCO, INC.
(Ci
(_y 3.3 C,ontainment Requirements for the Hypothetical r )
Accident Conditions From Chapter 1.0 and 2.0 the salient points are the permanent distortion of the closure lid and the temperature of the closure seals.
Since the closure seals have a higher temperature than the drain seals, and both are the same material, the limiting case is the closure seal.
i 3.3.1 Fission Gas Products (NOT APPLICABLE) 3.3.2 Release of Radioactive Materials (Contents)
For purposes of this analysis, it is assumed that there would be a one inch hole effective area in the cask seal lid, and the air volume within the cask would change three times per hour.
- Thus, there would be three conplete changes of air per unit of time and the volocity reactor would be integrated to infinity.
()
The potential source of airborne contamination would be from the corrosion products adhering to the sur-face of the non fuel' bearing components in th'e form of a film and loose particulate It should be noted that the materials which are placed in the cask are at all times in canisters for ultimate disposal.
There is, therefore, no possibility of leakage to the atmosphere.
- However, the assumption here is based on a system without canister and demonstrates that the airborne con-tamination levels are not in access of 10CFR20 li-miters for mixed corrosion and fission products.
The pick up of activity by transport has heen demon-
~
strated by Hestord, and Veselkin and Shakh as a con--
stant of the first order.
The constants for the following listed materials are the following:
Stainless Steel:
-2 Co-60 7 x 10
-2 Fe-59 6 x 10 O
3-3 ANEFCO, INC.
(_,)
Release of Radioactive Material (Contents) - con't Zircaloy
-3 CO-60 9 x 10 i
in fractions per second i
i j
Thus using the cask cavity volume of 1732.5 liters, we multiply the three air changes per hour or 5197.5 i
liters of air.
l The source strength ( f'/cm
- sec) is; l
10 Sv - 1.24 x 3.7 x 10 x pfy i
i N = Number,of curies f
v = Volume 10 4
Sv = 1.24 x 3.7 x 10 x 10 3
5519.5 x 10 5
Sv = 0.9 x 10 /hr.
5 Sv = 0.9 x 10 /60 x 60 Sv = 0.25 x 10 / min.
f 3
Sv = 0.417
/cm2 - sec.
-12 l
or 0.8 x 10 Ci/sec.
i
-6 or 0.9 x 10 uci/mi.
1 This level is far below any maximum permissible concentration to an unrestricted area in accordance with 10CFR20, 4
P Je i
i O l
3-4 ANEPCO, INC.
(%
V 3.4 Containment of RH-TRU Waste 3.4.1 Primary Vessel As indicated in Sect. ion 1.1.3.2 under the design i
criteria for the primary canister, a gas pressure drop leakage test will be conducted in accordance with the requirements of ANSI 14.5 to demonstrate that the final closure seals of the RH-TRU canister are effective.
The canister is equipped with a HEPA type filter which will retain all solids and permits venting of gases should venting be necessary.
1 3.4.2 Secondary Vessel It has been shown in Section 31312 i
that the maximum leak rate during accident I
conditions would be (3) three cask volumes per i
hour assuming a content of 104 curies,.which would l
release approximately 0.9 x 10-6 p0i/ min.
If such a leak rate were to occur for a one week
()
time interval, the total release of activity would be
~3 0.9 x 10-6 g g i; y 440 min 7 days, 9x 10 Jaci x
min day week week The A value for Pu 239 is 0.002Ci.
Therefore, the 2
containment capability within the AP-101 cask exceeds the requirements gf 10CFR71.51 with a i
safety factor of 2.2 x 10.
1 3-5 Rev 2 - 4/1/86 O
C f
3.4.3 Pressuriration of Containment It is assumed that an overpressure of 300 psig, produced by the RH-TRU. waste, is imposed on the cask c,avity.
This pressure will be contained within the cask by the inner shell, which will be braced by the lead and the outer shell as well as by the upper plate and 20 1 " - 12UNF x 2 " long hex bolts.
Considering the inner shell as the pressure vessel, the primary membrane stress is:
(Roark & Young p.448, case Ib) 1
= 300 psi
= 6720 psi-
.S
=
0 625 in m
Considering the bottom cavity plate as a simple supported plate, the maximum stress is:
(Roark & Young p. 363, case 10a)
J S,= 6(0.206)
= 1.236(300) psi (2.06 S,= 17,085 psi The closure lid, which is thicker, will have even lower stresses.
The twenty closure bolts will have to resist a load imposed by the 300 psi pressure on the 28" diameter cavity.
The pressure stress will be:
300 psi ( 7f ) (142) in2
= 6077 psi g
2 B
20 x 1.52 in At a temperature of 100*F, the allowable primary membrane stress is 20,000 psi (as shown in Table 1.3-1)
The allowable membrane plus bending stress is 28,000 psi and the allowable stress in the bolts is 105,000 psi.
These values exceed the calculated values of 6720 psi for the membrane stress, 23,800 psi for the membrane plus bending stresses, and 6080 psi for the bolt stress.
Therefore, the cask cavity"will withstand the 300 psi specification requirements of RH-TRU shipments.
O 3-6 Rev 2-4/1/86
3.4.4 Gas Generation in RH-TRU Waste v
Introduction The generation of gases, including hydrogen, in TRU wastes has been studied extensively.
In this evaluation, appropriate data from the literature has been applied to the packaging and transporta-tion system for RH-TRU waste in the cask.
The rates of total gas and hydrogen gewuation with-in the RH-TRU waste have been calculated, as have'
'the pressure consequences of such an occurrence Vithin the RH system.
For this evaluation, it is assumed that waste containers are overpacked int.o DOT 17C 55 gallon drums.
Three 55 gallon drums will fit into a 26" O.D. x 121"long waste canister which in turn will fit into the 28" ID The waste canister design includes a filtered vent, and the interior containers, including-the 55 gallon drums, are not pressure tight.
Therefore, no pressure barrier exists between the actual waste l
and the cask which is assumed to be pressure-J tight for this evaluation.
Gas Generation Mechanisms The gas generation mechanisms,used in this evalu-ation, as identified in the literature, include radiolysis,. bacterial decomposition, thermal de-gradation and corrosion.
The radiolytic gas generation rates are given by:
Rate = A x F xf x G Where A = Total Activity for Radiation type under Consideration F = Average Energy per Disintegration (MeV/ dis) f = Fraction of energy absorbed by material G = Number of Gas Molecules Produced per 100eV absorbed For Alpha radiolysis, assuming that 1000 Ci at an average energy of 5MeV and a G value of 1.4 are O
present in a load, 1.55 x 10 moles /hr are generated.
2 3-7 Rev 2 - 4/1/86
7 o
f For Beta radiolysis of water and hydrocarbons,
(
assuming that 900 Ci at an average energy of 0.28MeV and a G value of 0.45 for water and 1.4 for hyh ocarbons are present in a load, 7.6 x 10-4 I
moles /hr are generated.
Assuming a maximum temperature of 100*C, it can j
be estimated from the literature that 1.5 x 10-2 moles /hr are generated by thermal degeneration.
Bacterial and corrosion gas generation are not credible or measureable for the conditions I
i assumed above.
The gas generation by the above mechanisms have been estimated to be about 3.14 x 10-2 moles /hr.
Pressure Build-up
~
In order to determine a pressure build-up, it is J
necessary to assume a void volume which will be l (q present in the containers, the drums, the canister, and the transportation cask.
For this conservative evaluation, it was assumed that 50% of the drum volume was void, and that there is a 0.5 inch clearance between the transport cask and the canister.
The absolute pressure in the cask at any time is:
Po [n +5t) Tt o
pt, g g
Where P = Absolute Pressure n = Number of moles 6 = Gas Generation rate (moles / time)
T = Absolute Temperature t = elapsed time sub o= at time 0 O
uh t - et time e assuming that T
= 298'K, Tt = 373*K, Po = 14.7 psia o
f i
3-8 Rev 2 - 4/1/86
{
1 i
(
and that the gas generation rate is 3.14 x 10-2 moles /hr The absciute pressure in the cask will be 33.1 psia after one month and 196.6 psia after one year.
Calculations were performed for the capability of the AP-101 cask to contain RH-TRU waste under pressure.
Those calculations showed a capability to retain a pressure build-up of 300psig, which will be extremely conservative when it is considered I
that it would take a year to reach a pressure'less than 200psig. See Scction 3.4.3.
]
O
.V 3-9 Rev 2 4/1/86
()
1, I
l O
'3 4 5
=v 2= tioa==== rv It is shown in 3.4.1 above that the primary vessel is designed to retain all solid RH-TRU wastes that will be loaded into the canister.
The canister is vented through a HEPA filter which will release the gases should gas.
release occur.
In Section 3.4.2, it is shown that the design of the J
AP-101 cask will release less than the allowable A2 quantities of radioactivity.
Section 3. 4.3 demonstrates that the design of the AP-101 cask is capable of resisting a pressure of 300 psig which is the maximum pressure to be released from the RH-TRU canister.
Consequently, the combination of the RH-TRU waste canister packaged in the AP-101 transport cask provides adequate containment for the RH-TRU waste.
O E
l 3-10 Rev 2 - 4/1/86 O
3.5 AP-101 CASK CONSIDERATIONS FOR RH_TRU WASTE O
3.5.1 Hypothetical Release Considerations The AP-101 cask willbe sealed and leak tested to assure that there is no leak, using a detector with a minimum sensitivity of 1 x 10-3atm - h
, in accordance with ANSI 14.5.
If it is assumed that a leak occurs during a transport, at a rate of 1 x 10-3 [c, the total leak for a duration of one week will be:
5 e
cc 10-3 x
6.048 x 10
= 604.8 sec The maximum activity that will be transported in the AP-101 cask will be 100001.
It has been shown* that only 0.5% of the RH-TRU waste activity is present as leakable, respirable fines.
Further, the canister vent HEPA filter has 99.7%
efficiency factor for' O.3u particulate.
Combining the above i
factors, the total activity that will be available to the cask interior will be:
1000Ci x 5 x 10-3 x 3 2-10-3 = 0.015Ci y
The volume of the canister, which has a 26"OD and is 121" high is:
3 7f (26")2 (121")
= 37.18 ft 4
1728 The volume of the AP-101 cavity, which is 28"ID and 167" high is:
i 3
Y (28")2 (167")
59.51 ft
=
4 1728 Given the total activity of 0.015Ci is distributed in the void volume of the cask, the concentration of activity ist 3
5 (59.51 - 37.18)ft x 2.832 x 104 {3
= 6.32 x 10 cc 0.015Ci
= 2.37 x 10-8 5
6.32 x 10 cc for a duration of one Assuming a leak rate of 1 x10-3 ce week, the total activity thatwouf8cbe leaked is:
O So4.8gx2.37x10-8c; 1.43 x 10-5 g
- Warrant, M.M., " Report of the RH-TRU Characteristics Interface Working Group", April 30, 1985.
3-11 Rev 2 - 4/1/86
Assuming a most restrictive A value of 0.002, a safety 2
oU
-3
.f,j3
= 140 is available.
factor of yg_3 3.5.2 Cask Dunnage The nominal RH-TRU canister dimensions are 26"OD x 121" long. (Ref. Dwg.)
This canister will be positioned in the AP-101. cask whose cavity dimensions are 28" ID x 167" long.
Calculations have been performed to assure that the potential energy developed by the movement of the canister during transportation of the canister within the cask will be absorbed by an installed buffer and will not affect the cask.
For that purpose, a cylinder, fabricated from a honeycomb material will be installed in the AP-101 cask to absorb the energy.
The max. mum weight of the canister (in conformance with the AP-101 Certificate of Compliance) is 10,000 lbs.
The maximum distance that the canister can travel within the AP-101 cask is the difference between the length of the cavity and the length of the canister.
The maximum
)
acceleration that the canister will attain is 10g along the direction in which the package travels, equivalent to the standard applied for tie-down forces in 10CFP 71.45, dc thus the maximum energy that could be developed would be:
10 x 10,000 lbs x 46 in. = 4,600,000 in-lbs.
The stress required for the deformation of the honeycomb material that will be employed is 1600 h /in.
Given the OD of the honeycomb cylinder as 27.5 inches, then the energy absorption capacity of such a cylinder
(
is:
i D
2 x 1 inch = 950,300 "
(27.5)2in 1600 2/in x
The maximum potential energy of the canister would there-f fore, be absorbed in 0
= 4.84 inches or less than 5 inches of a 27.5 inch diameter cylinder of honeycomb material.
A 45" long cylinder which will be installed to serve as dunnage, will limit the movement of the RH-TRU canister and will have excess capability to absorb any potential energy developed. ( Ref. DWG SZ-5) o a
3-12 Rev 2 - 4/1/86
~,
4.1 SHIELDING EVALUATION P
' SQ The approach used in these calculations can be found
()
in the " Reactor Shielding Design Manual" by Theodore Rockwell III.
8-
- 4_* f-r j
I
, O N;;s-s 1
p- ~
- -> P
'~ N j:L7 s s__
n i
~
\\-
r -.
At P
/ = BSv(Ro)
F (0,b)
@O
=O y
2 2 (a + Z)
The only shielding remaining is the 1 1.2 inch outer shell plus the 5/8 inch inner shell which is equal to 2 1/8 inch steel shielding.
The distance "a" assuming that the lead thickness is replaced by void volume is:
l
{])
a = 1 + 1/2 + 1 + 3 a = 5.5 in. = 14.0 cm.
Ro = 54/2 in. = 68.5 cm.
h = 0.45 in. = 1.14 cm.
The thickness of shield "t"
f t = 1.5 in. = 3.82 cm. (steel)
I f
where f = photon flux (photons /sq. cm. - sec. )
I Sv = Source strength (photons / cu. cm. - sec.)
B = build-up factor Z =.self attenuation thickness To determine Z we compute:
a 14.0 l'
ji Ro 68.5 a
=.20
.o Ro o
li i
4-1 ANEPCO INC.
shielding Evaluation (con ' t) o
'FN The source material is assumed to have the properties
(_)
of water.
Thes s of water at 1.25 MEV is obtained
~
u frcm the graph on page 448 of Rockwell.
4c s =.064 j
.064 (14. 0 + 68.5)
/(s (a + Ro)
=
.064 (82.5)
=
44 s (a + Ro) = 5. 3 j
From the graph on page 362 of Rockwell, the parameter "m"
is:
l m = 0. 99 for a/Ro =. 20,/4 s (a + Ro) = 5,3 Before we can determine "Z" we must know bf by = jut where A = the microscopic cross section of the shield jt = thickness of shield
'( )
From Rockwell pate 447 the value ofA for steel at 1
1 25 MEV is:
j/(=.391 r
b
=.391 (3.82) b
= 1.49 y
With this value of b and a/Ro we can find the parameter (1/m)jgsZ from the graph on page 363 of Rockwell.
(1/m)j sZ = 2.56 for a/Ro =.20, by = 1.49 q
i I
Z = 2.56 (1/m)jks Z = 2.56 (1/0.99).064
= 2.56
.065
{
Z = 39.4
(. )
4-2 ANEFCO, INC.
Shielding Evaluation (con ' t)
A To find the angle 6:
P i4 1 r__
tan O = 1.14/2
-(14. 0 + 39. 4 )
= 0.57 53.4 tan G =.0107 e = 0'37' b
=b
+ p sZ
= 1.49 +.064 (39.4) i
= 1.49 + 2.52 b = 4.01 2
From the graph on page 385 of Rockwell with b
= 4.01 2
O = 0'37'
-4 F (0,b) = 2.5 x 10 The build-up factor for steel is:
Sh.X+Ae4 /4%
4 B=Ae From the graph on page 422 of Rockwell at 1.25 MEV:
A
= 8.1 y
A2 = -7.1 d,
=.0835 c(2
=.034 f.(, x = (. 391) (3. 8 2) = 1.49 O
l l
4-3 ANIEFCO, INC.,
1 C
Shielding Evaluation (Con 't) q' u, x = - (.0835) (1.49)
/
g g,x =.124 jg, x - - (. 03 4 ) (1. 4 9)
- % /4x =
.051
~
B = 8.1 e *
- 7.1 e
= 8.1 (1.134) - 7.1 (.95)
= 9.20
'6.75 B = 2.45 4.2 Gamma Flux l
The maximum dose rate on the cask surface at any point due to the hypothetical accident is 1000 mr/hr or 1.0 R/hr.
The dose "D'~ is related to the gamma flux by the relationship:
[
D-fK I
(
where K is the convepsion factor for photons /sq.cm - see to R/hr:
f=D/K D = 1.0 R/hr K = 2.3 x 10-6
@ l 25 MEV f=1.0 2.3 x 10-6 6
3 f=.435x10 5
$ = 4.35 x 10 since:
f=BSV (Ro),
F (0,b )
2 2 (a + z) c0 e
4-4 ANEPCO INC.
u
.=
Shielding Evaluation (Con ' t)
O Sv = d 2 (a' + E)
B (Ro)
F (0,b) 5 Sv = (4.35 x 10 ) 2. 0 (14. 0 + 39.4 )
2.45(68.5)2 (2.5 4)
(4.35 x 10)
(106.8)
=
(1.15 x 109)
(2.5 x 10-4) 464 x 10
=
2.88 7
Sv = 1.62 x 10 photons / cubic cm -sec 4.3 Side Drop Gamma Shielding i
For the side drop case we lose 1.0 inch of lead shielding.
Repeating the above calculations for this case:
/
W
~
RN M
- D i 'x i
Io '
i r-- - -- p '_. 2,P
\\ e+,
^
I l
/
V' y
k j
Ro = 54/2 = 68.5 cm.
h = 77 inch = 195 cm.
t = 2 inch lead + 1.5 inch steel = 2.75 inch lead (ORNL-NSIC - 68 Fig. 7.3) t = 7.0 cm.
a = 5.5 in. - 1.0*in. = 4.5 in a = 11.4 cm.
'O l
4-5 ANEPCO, INC.
L
Shielding Evaluntion (con ' t)
'F a
= 11.4
(]
Ro 68.5 a
=.166
)
Ro t
,4s =.064
'< s (a + Ro) =. 064 (11. 4 + 68. 5)
.064(79.9)
~
=
I ps (a + Ro) = 5.12 l
m =.97 t
b=
t j< =. 6 81 t = 7.0 l
b,=.681 (7. 0) j b
b,= 4.77 (1) sZ = 2.95 (m)
Z = 2.95 (1/m) u s
= 2.95 (1/. 97 ).064) t
= 2.95 (1. 03 ) (. 064)
L
= 2.95 7066 Z = 44.6 1%
P LO
~n.
,i t
ANEFCO INC.
4-6 t
Shielding Evaluation (con't)
O tan 0 = 195/2.0 g'-]J km (11.4 + 44.6) 97.5 j
=
56.0 i
tan 0 = 1.74 t
0 = 60'53' l
b,= b,+,usz
= 4.77 +.064 (44.6)
= 4.77 + 2.86 b,= 7.63 (0,b )= 2.1 x 10-4 F
2 Build-up factor for lead
-hoX Ae h
- I
~
, (
B = Ae
+
A = 2.53 A = l-A I
y A = -1.53 A = l-A L
L 6,=
.05 ek,=.15 p,x = 4.77
-/nox = -(.05) (4.77) c y
_d,,a,x =.238
. c4 j, x = - (.15) (4.77) o
. cy fu. x =
.714 l
\\
l (O
4-7 ANEFCO, INC.
i i
7 Shiolding Evaluation (con't)
(h1 B = 2.53 e *238 1.53 e
- 714
= 2.53 (1.268) - 1.53 (.49)
=, 3.23
.75 B = 2.48 5
0_= 4.35 x 10 for D = 1.0 R/hr.
0 = B Sv Ro2 F (0,b)
~
2 (a + Z)
Sv = 0 2 (a + Z )
2 (F (0,b)]
B Ro (4.35 x 10)5 2.0 (11. 4 + 4 4. 6)
=
2
-9 2.48 (68.5)
(2.1 x 10)
= 4.35 (2.0) (56) x 10
-4 2.48 (4700) (2.1) x 10 S
= 488 x 10
'f4400 x 10 A 7
= 4.88 x 10 2.44 Sv = 2.0 x 10' photons / cubic cm.
sec.
The previous case is governing (1.6x103 Since the loading will be below the governing value the shielding during the accident is adequate.
'O 4-8 ANEFCO, INC.
_-