potential production of molybdenum-99 · 2014. 10. 1. · page | ii abstract in this study, the...
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DEVELOPMENT OF A 37-ELEMENT FUEL BUNDLE FOR THE PRODUCTION OF
MOLYBDENUM-99 IN CANDU POWER REACTORS
By
Jawad Haroon
A Thesis Submitted in Partial Fulfillment
of the Requirements for the Degree of Master of Applied Science
In
The Faculty of Energy Systems and Nuclear Science
Nuclear Engineering
University of Ontario Institute of Technology
August 2014
© Jawad Haroon, 2014
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Abstract
In this study, the potential use of CANDU power reactors for the production of
Mo-99 is assessed. Five different modifications of a 37-element fuel bundle that could
be used for the production of Mo-99 in existing CANDU type power reactors are
explored. Since Mo-99 is generated by the fission of U-235 with a fission yield of 6.1%,
the proposed designs use enriched uranium in the Mo-99 producing fuel pins. The
challenge lies in designing a fuel that is able to produce significant quantities of Mo-99
while having similar neutronics and thermalhydraulic characteristics to the standard
CANDU fuel.
The proposed designs, when irradiated in the peak power channel of a CANDU
core, are shown to produce significant quantities of Mo-99 while maintaining the
necessary reactivity and power rating limits. The total Mo-99 production activities are
found to be approximately 2335, 2297, 2336, 4131 and 4268 six-day Curies per bundle
for Designs 1 to 5, respectively. The yield corresponds to approximately 19% (for
Designs 1, 2 and 3) and 34% (for Designs 4 and 5) of the world weekly demand for
Mo-99. A production cycle of 6 bundles per week (for Designs 1, 2 and 3), or 3 bundles
per week (for Designs 4 and 5) can meet the global demand of Mo-99 medical isotopes.
Keywords: Medical Isotopes, CANDU, DRAGON Code, Molybdenum-99, Six-Day Curies,
Infinite Multiplication Factor, Linear Heat Rating, Fuel Centreline Temperature
Page | iii
Acknowledgement
I am grateful to my research supervisor Dr. Eleodor Nichita for giving me this
opportunity to research under his guidance. I sincerely thank him for his valuable advice
and confidence in my abilities throughout my Masters. I thank him for all the guidance
and information he provided that allowed me to start off this project, and helping me
every time I felt lost.
A special thank you to Wargha Peiman, who is a PhD candidate at the University
of Ontario Institute of Technology for his help with the DRAGON code and the many
interesting discussions we had on deciphering code manuals.
I would like to dedicate this thesis to my mother and father, Sarwat Siddiqa and
Haroon-ur-Rashid, who from an early age encouraged me to pursue my interest in
science and engineering. Thank you for all the encouragement along the way and for the
value placed on family. Thank you to my wonderful sister, Saba Haroon, who was there
for me throughout the writing process to help me proofread and give suggestions. I
would like to thank all my family and friends for their love and support throughout my
Masters, in particular, Brooke Smyth for many years of happiness and continued love,
support and inspiration.
It has been an honour and a pleasure, thank you all.
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Table of Contents
ABSTRACT ........................................................................................................................................................ II
ACKNOWLEDGEMENT ................................................................................................................................ III
TABLE OF CONTENTS .................................................................................................................................. IV
LIST OF ACRONYMS .................................................................................................................................... XII
CHAPTER 1 INTRODUCTION ...................................................................................................................... 1
1.1 INTRODUCTION TO NUCLEAR MEDICINE .................................................................................................... 3
1.1.1 WHAT IS NUCLEAR MEDICINE? .............................................................................................................................. 3
1.1.2 MEDICAL ISOTOPES AND DISEASES ....................................................................................................................... 4
1.1.3 MOLYBDENUM-99/TECHNETIUM-99M: THE MOST COMMON RADIOISOTOPE ........................................... 5
1.2 DEMAND FOR MOLYBDENUM-99 ............................................................................................................... 5
1.3 THE BIG FIVE MEDICAL ISOTOPE PRODUCING REACTORS ....................................................................... 7
1.4 INTRODUCTION TO RADIOISOTOPE PRODUCTION IN NUCLEAR REACTORS ......................................... 11
1.5 ALTERNATIVE METHODS FOR PRODUCING MOLYBDENUM-99 ............................................................ 12
1.5.1 PHOTO-FISSION PROCESS 238U(Γ,F)99MO ......................................................................................................... 12
1.5.2 NEUTRON ACTIVATION OF MOLYBDENUM-98 ................................................................................................. 12
1.5.3 NEUTRON EMISSION FROM MOLYBDENUM-100 ............................................................................................. 13
1.6 RADIOACTIVE DECAY OF MOLYBDENUM-99/TECHNETIUM-99M ....................................................... 14
1.7 CONSIDERATIONS IN THE PRODUCTION OF MOLYBDENUM-99 IN NUCLEAR REACTORS .................... 16
1.7.1 MOLYBDENUM-99 TARGET PROCESSING TECHNIQUES ................................................................................. 18
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1.7.2 TECHNETIUM-99M GENERATORS....................................................................................................................... 21
1.7.3 SPENT FUEL CONSIDERATIONS ........................................................................................................................... 23
1.8 CANDU REACTORS AND THE DRAGON LATTICE CODE ...................................................................... 26
1.8.1 USING CANDU REACTORS FOR MOLYBDENUM-99 PRODUCTION ............................................................... 26
1.8.2 THE DRAGON CODE ............................................................................................................................................ 30
CHAPTER 2 PRODUCTION OF MOLYBDENUM-99 IN NUCLEAR REACTORS: PRESENT AND
FUTURE ........................................................................................................................................................... 33
2.1 CURRENT MOLYBDENUM-99 SUPPLY CHALLENGES .............................................................................. 34
2.2 CONVERSION OF MOLYBDENUM-99 TARGETS FROM HIGHLY-ENRICHED URANIUM TO LOW-
ENRICHED URANIUM ....................................................................................................................................... 35
2.3 NEW PRODUCERS OF MOLYBDENUM-99 WORLDWIDE ........................................................................ 37
2.4 MOLYBDENUM-99 PRODUCTION IN POWER REACTORS ....................................................................... 38
CHAPTER 3 METHODOLOGY FOR THE DEVELOPMENT OF A MOLYBDENUM-99
PRODUCING 37-ELEMENT FUEL BUNDLE DESIGN ........................................................................... 41
3.1 DESIGN OBJECTIVES .................................................................................................................................. 41
3.2 DESIGN PLAN AND STRATEGY .................................................................................................................. 42
3.2.1 SATISFYING DESIGN REQUIREMENTS ................................................................................................................. 45
3.3 REACTOR OPERATING CONDITIONS AND ASSUMPTIONS ....................................................................... 51
3.3.1 REACTOR FUELLING CONSIDERATIONS ............................................................................................................. 52
3.4 DESIGN OPTIONS AND METHODOLOGY ................................................................................................... 54
3.4.1 METHOD FOR CALCULATING THE LINEAR HEAT RATING ............................................................................... 57
3.4.2 METHOD FOR CALCULATING THE RADIAL TEMPERATURE PROFILE ............................................................ 60
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3.4.3 METHOD FOR CALCULATING THE MASS AND ACTIVITY OF MOLYBDENUM-99 PRODUCED ..................... 69
CHAPTER 4 ASSESSMENT RESULTS AND DISCUSSION ................................................................... 73
4.1 TASK 1 - COMPARISON OF INFINITE MULTIPLICATIVE CONSTANTS ..................................................... 78
4.2 TASK 2 - COMPARISON OF LINEAR HEAT RATING ................................................................................. 85
4.3 TASK 3 - COMPARISON OF RADIAL TEMPERATURE PROFILES .............................................................. 92
4.4 MASS AND ACTIVITIES OF MOLYBDENUM-99 ...................................................................................... 113
CHAPTER 5 CONCLUDING REMARKS AND FUTURE WORK ........................................................ 117
REFERENCES ............................................................................................................................................... 120
APPENDICES ............................................................................................................................................... 135
APPENDIX A – POTENTIAL PRODUCERS OF REACTOR PRODUCED MOLYBDENUM-99............................ 135
A.1 MULTIPURPOSE APPLIED PHYSICS LATTICE EXPERIMENT (MAPLE) .......................................................... 135
A.2 AQUEOUS HOMOGENEOUS REACTOR (AHR) ..................................................................................................... 137
A.3 OPEN POOL AUSTRALIAN LIGHT-WATER (OPAL) REACTOR ........................................................................ 138
A.4 JULES HOROWITZ REACTOR (RJH) ...................................................................................................................... 140
A.5 CHINA ADVANCED RESEARCH REACTOR (CARR) ............................................................................................ 142
A.6 UNIVERSITY OF MISSOURI RESEARCH REACTOR CENTER (MURR) .............................................................. 143
A.7 SANDIA NATIONAL LABORATORIES (SNL) ........................................................................................................ 144
A.8 OTHER POTENTIAL SUPPLIERS OF REACTOR PRODUCED MOLYBDENUM-99 .............................................. 148
A.9 NEW APPROACHES IN DIAGNOSTIC NUCLEAR MEDICINE ................................................................................ 150
APPENDIX B – MATERIALS, LATTICE SPECIFICATIONS AND IMPORTANT PARAMETERS FOR 37-ELEMENT
CANDU FUEL BUNDLE CALCULATIONS ....................................................................................................... 151
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APPENDIX C – INITIAL ESTIMATES OF ENRICHED FUEL REGION THICKNESS AND PIN RADIUS FOR UO2
AND U-METAL FUEL DESIGNS BASED ON URANIUM MASS BALANCING .................................................... 153
Page | viii
List of Figures
Figure 1-1: Approximate Global Demand for Molybdenum-99 ............................................................................................ 7
Figure 1-2: Principal Decay Scheme of Molybdenum-99 ...................................................................................................... 16
Figure 1-3: Buildup of Molybdenum-99 Radioactivity for a Neutron Flux Typical of a CANDU-6 ....................... 18
Figure 1-4: Global Supply Chain of Molybdenum-99 and Utilization Schematics ....................................................... 20
Figure 1-5: Decay of Molybdenum-99 and Buildup of Technetium-99m Activity after Each Elution,
Calculated for 7 Days .......................................................................................................................................................................... 22
Figure 1-6: Generic Flow Chart of Waste Streams Generated from Molybdenum-99 Production ........................ 25
Figure 1-7: CANDU Reactor Face ................................................................................................................................................... 28
Figure 1-8: A Typical CANDU Fuel Channel................................................................................................................................ 29
Figure 3-1: A Pictorial Representation of the Proposed Designs Assessed for Molybdenum-99 Production .... 44
Figure 3-2 37-Element CANDU Fuel Bundle and the Infinite Lattice Cell Representation of Design 2.............. 57
Figure 3-3: A Plot of UO2 Thermal Conductivity Showing Variation Due to Temperature ..................................... 65
Figure 4-1: Radial Pin Power Profile for Reference CANDU 37-Element Bundle ........................................................ 74
Figure 4-2: Reference CANDU 37-Element Bundle Radial Temperature Profile of Ring 4 Pin Using IAEA and
Constant Thermal Conductivity for UO2 ...................................................................................................................................... 77
Figure 4-3: Design 1 Unitcell Lattice k-infinity Versus Variations in Radius of Enriched Central Target
Region (Fuel Pin Radius 6.075 mm) .............................................................................................................................................. 80
Figure 4-4: Design 2 Unitcell Lattice k-infinity Versus Variations in Thickness of Enriched Annular Target
Region (Fuel Pin Radius 6.075 mm) .............................................................................................................................................. 81
Figure 4-5: Design 3 Unitcell Lattice k-infinity Versus Variations in Thickness of Enriched Annular Target
Region (Fuel Pin Radius 4.266 mm) .............................................................................................................................................. 82
Figure 4-6: Design 4 Unitcell Lattice k-infinity Versus Variations in Thickness of Enriched Annular Target
Region (Fuel Pin Radius 6.075 mm) .............................................................................................................................................. 83
Figure 4-7: Design 5 Unitcell Lattice k-infinity Versus Variations in Thickness of Enriched Annular Target
Region (Fuel Pin Radius 4.266 mm) .............................................................................................................................................. 84
Figure 4-8: Design 1 Bundle Radial Pin Power Profile ........................................................................................................... 87
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Figure 4-9: Design 2 Bundle Radial Pin Power Profile ........................................................................................................... 88
Figure 4-10: Design 3 Bundle Radial Pin Power Profile ........................................................................................................ 89
Figure 4-11: Design 4 Bundle Radial Pin Power Profile ........................................................................................................ 90
Figure 4-12: Design 5 Bundle Radial Pin Power Profile ........................................................................................................ 91
Figure 4-13: Design 1 Radial Temperature Profile of Ring 4 Pin Using IAEA Thermal Conductivity for UO2 . 97
Figure 4-14: Design 1 Radial Temperature Profile of Ring 4 Pin Using a Constant Thermal Conductivity for
UO2 (0.024 W/cm∙K) ............................................................................................................................................................................ 98
Figure 4-15: Design 2 Radial Temperature Profile of Ring 4 Pin Using IAEA Thermal Conductivity for
UO2 ........................................................................................................................................................................................................... 101
Figure 4-16: Design 2 Radial Temperature Profile of Ring 4 Pin Using a Constant Thermal Conductivity for
UO2 (0.024 W/cm∙K) ......................................................................................................................................................................... 102
Figure 4-17: Design 3 Radial Temperature Profile of Ring 4 Pin Using a Constant Thermal Conductivity for
U-Metal (0.43 W/cm∙K) ................................................................................................................................................................... 105
Figure 4-18: Design 4 Radial Temperature Profile of Ring 4 Pin Using IAEA Thermal Conductivity for
UO2 ........................................................................................................................................................................................................... 108
Figure 4-19: Design 4 Radial Temperature Profile of Ring 4 Pin Using a Constant Thermal Conductivity for
UO2 (0.024 W/cm∙K) ......................................................................................................................................................................... 109
Figure 4-20: Design 5 Radial Temperature Profile of Ring 4 Pin Using a Constant Thermal Conductivity for
U-Metal (0.43 W/cm∙K) ................................................................................................................................................................... 112
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List of Tables
Table 1-1: Worldwide Production Capacity of Molybdenum-99 ([11], [12], [13], [14]) ............................................. 9
Table 1-2: Small-Scale Producers of Molybdenum-99 in 2011 ([8], [11], [14]) ........................................................... 10
Table 1-3: Status of CANDU reactors and CANDU-Derivatives in 2014 ([28], [29]) .................................................. 27
Table 4-1: Reference CANDU 37-Element Bundle Data Structures for Radial Pin Power Profile
Calculations............................................................................................................................................................................................. 74
Table 4-2: Reference CANDU 37-Element Bundle Normalized Heat Density and Linear Power Rating in Ring
4 Sub-regions .......................................................................................................................................................................................... 75
Table 4-3: Reference CANDU 37-Element Bundle Numerical Integration Results Using IAEA and Constant
Thermal Conductivity for UO2 .......................................................................................................................................................... 76
Table 4-4: Design 1 Unitcell Lattice k-infinity for Variations in Radius of Enriched Central Region .................. 80
Table 4-5: Design 2 Unitcell Lattice k-infinity for Variation in Thickness of Enriched Annular Region ............ 81
Table 4-6: Design 3 Unitcell Lattice k-infinity for Variation in Thickness of Enriched Annular Region ............ 82
Table 4-7: Design 4 Unitcell Lattice k-infinity for Variation in Thickness of Enriched Annular Region ............ 83
Table 4-8: Design 5 Unitcell Lattice k-infinity for Variation in Thickness of Enriched Annular Region ............ 84
Table 4-9: Design 1 Data for Radial Pin Power Profile Calculations ............................................................................... 87
Table 4-10: Design 2 Data for Radial Pin Power Profile Calculations ............................................................................. 88
Table 4-11: Design 3 Data for Radial Pin Power Profile Calculations ............................................................................. 89
Table 4-12: Design 4 Data for Radial Pin Power Profile Calculations ............................................................................. 90
Table 4-13: Design 5 Data for Radial Pin Power Profile Calculations ............................................................................. 91
Table 4-14: Thermophysical Properties of Coolant Using NIST REFPROP [46] ........................................................... 94
Table 4-15: CANDU Specific Important Heat Transfer Parameters [46] ........................................................................ 94
Table 4-16: Design 1 Normalized Heat Density and Linear Power Rating in Ring 4 Sub-regions ....................... 95
Table 4-17: Design 1 Numerical Integration Results Using IAEA and Constant Thermal Conductivity for
UO2 .............................................................................................................................................................................................................. 96
Table 4-18: Design 2 Normalized Heat Density and Linear Power Rating in Ring 4 Sub-regions ....................... 99
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Table 4-19: Design 2 Numerical Integration Results Using IAEA and Constant Thermal Conductivity for
UO2 ........................................................................................................................................................................................................... 100
Table 4-20: Design 3 Normalized Heat Density and Linear Power Rating in Ring 4 Sub-regions .................... 103
Table 4-21: Design 3 Numerical Integration Results Using Constant Thermal Conductivity for U-Metal ..... 104
Table 4-22: Design 4 Normalized Heat Density and Linear Power Rating in Ring 4 Sub-regions .................... 106
Table 4-23: Design 4 Numerical Integration Results Using IAEA and Constant Thermal Conductivity for
UO2 ........................................................................................................................................................................................................... 107
Table 4-24: Design 5 Normalized Heat Density and Linear Power Rating in Ring 4 Sub-regions .................... 110
Table 4-25: Design 5 Numerical Integration Results Using Constant Thermal Conductivity for U-Metal ..... 111
Table 4-26: Design 1 Molybdenum-99 Production Results ............................................................................................... 114
Table 4-27: Design 2 Molybdenum-99 Production Results ............................................................................................... 114
Table 4-28: Design 3 Molybdenum-99 Production Results ............................................................................................... 114
Table 4-29: Design 4 Molybdenum-99 Production Results ............................................................................................... 115
Table 4-30: Design 5 Molybdenum-99 Production Results ............................................................................................... 115
Table A-1: Potential Future Suppliers of Reactor Produced Molybdenum-99 [13] ................................................. 149
Page | xii
List of Acronyms
ACRR Annular Core Research Reactor
AECL Atomic Energy of Canada Limited
AHR Aqueous Homogeneous Reactor
ANSTO Australian Nuclear Science and Technology Organization
B&W Babcock & Wilcox
CANDU CANada Deuterium Uranium
CARR China Advanced Research Reactor
CEA Atomic Energy Commission
CHF Critical Heat Flux
CNSC Canadian Nuclear Safety Commission
DOE Department of Energy
FDA Food and Drug Administration
HEU Highly-Enriched Uranium
HFR High Flux Reactor
IAEA International Atomic Energy Agency
Page | xiii
LEU Low-Enriched Uranium
MNR McMaster Nuclear Reactor
MURR University of Missouri Research Reactor
NRU National Research Universal
NU Natural Uranium
OPAL Open Pool Australian Light-Water Reactor
RJH Jules Horowitz Reactor
SNL Sandia National Laboratories
SNM Society of Nuclear Medicine
US-NRC Unites States Nuclear Regulatory Commission
WLUP WIMS-D Library Update
Page | 1
Chapter 1
Introduction
In nuclear medicine, radioactive nuclides are used to obtain functional
information about a patient’s organs and to diagnose and treat various medical
conditions [1]. The most common radioisotope used in nuclear medicine is
technetium-99 (Tc-99m), which is produced through the radioactive decay of
molybdenum-99 (Mo-99). Tc-99m is used in approximately 30 million procedures per
year, accounting for 80% of all nuclear medicine procedures worldwide [2].
Mo-99 is most commonly and effectively generated in nuclear reactors by the
fission reaction of U-235 with a yield of 6.1% [3]. Mo-99 production in fission reactors
is usually achieved by irradiation of specially designed highly-enriched uranium (HEU)
targets located inside irradiation rigs positioned at special high-flux sites in the core.
These HEU targets typically have a U-235 enrichment of 90 wt% or higher. Although
some Mo-99 is produced in natural uranium (NU), the NU fuel composition is not suitable
for producing significant quantities of Mo-99 since the ratio of Mo-99 yield to fuel volume
processed is generally low. Therefore, the use of enriched fuel is desirable from the
perspective of Mo-99 production.
When uranium is enriched to less than 20% by weight of U-235, it is considered
low-enriched enriched uranium (LEU). Concerns over weapon proliferation and nuclear
security have led to advanced discussions between experts of the field with the aim of
using LEU instead of HEU as reactor fuel and target material.
Page | 2
As of 2014, the National Research Universal (NRU) reactor in Chalk River,
Ontario, produces approximately 40% of the global demand for Mo-99 [4]. The NRU is
57 years old and is scheduled to cease Mo-99 production in the year 2016. Consequently,
alternative production methods and radioisotope production facilities need to be
developed. One possibility is to irradiate specially designed fuel in the operating
CANDU®1 reactors; this is the main driver of the work presented in this thesis.
A CANDU reactor with its pressure channel design and its ability to fuel online
has the potential to produce large quantities of Mo-99, while maintaining its power
production targets. The production and extraction of Mo-99 is not possible in most other
power plants due to batch fuelling. The online refuelling capabilities in CANDU, with its
flexible and compact fuel design give CANDU reactors an edge over pressure-vessel light
water reactors which are generally refuelled in batches every 18 to 24 months.
The goal of this thesis is to evaluate various modified 37-element fuel bundles
specifically made for CANDU reactors with the intent to generate a significant portion of
the world’s demand for Mo-99 without significantly changing the physics or fuel bundle
safety characteristics. Several variations of the 37-element fuel bundle are analyzed
using the DRAGON lattice code. Strict design acceptance criteria are used, consisting of
close proximity of the fresh fuel k-infinity value to that of the reference CANDU bundle
1 CANDU is a trademark of Atomic Energy of Canada Limited used under licence by Candu Energy
Inc.
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(Δρ < 1 mk) and maintaining existing margins to linear heat rating limits. An assessment
of the fuel centreline temperature is also performed for the modified fuel bundle pins.
The strict design constraints allow the station to maintain existing operating
practices and eliminate the need for supplemental fuel safety analysis or full core
neutronics calculations.
1.1 Introduction to Nuclear Medicine
1.1.1 What is Nuclear Medicine?
Nuclear medicine uses small quantities of unstable nuclei administered to a
patient to study the function of specific organs in the body or to treat tumours and other
diseases ([1], [4]). The field of nuclear medicine can be divided into two branches:
diagnostics and therapeutics.
Diagnostics: A radiopharmaceutical consisting of a radioisotope bound to a
substrate is administered to a patient. The substrate is what governs the distribution of
the radiopharmaceutical in the body and is chosen such that it is predominantly
accumulated in the organ that needs to be investigated. The amount of accumulation in
the specific organ gives information about the health and function of the organ. The
gamma-emitting radioactive isotopes is what allows the distribution of the
radiopharmaceutical to be visualized using an external detector which produces a
diagnostic image. Images are then analyzed to detect partial or excessive absorption of
Page | 4
the isotope as an indication of organ malfunction [4]. Nuclear medicine imaging
provides a view of the position and concentration of the radioisotope which depends
primarily on an organ’s functioning rather than on its anatomy.
Therapeutics: Radioisotopes are injected into a patient in higher doses. The
isotopes emit very energetic photons or particles which can destroy targeted cells such
as cancer cells.
1.1.2 Medical Isotopes and Diseases
Medical isotopes are used routinely in the diagnosis and treatment of various
diseases at hospitals and radiation clinics. The following list includes, but is not limited
to some of the health conditions where various medical isotopes are used for monitoring
and evaluation [2]:
Heart disease
Level of functioning of brain, heart, lungs, kidneys and other organs
Tumours
Progression of cancer – spreading to bones
Hormonal disorders, ex. thyroid disease
Over hundreds of radiopharmaceutical products are used at hospitals and
radiation clinics in North America every day. About 95% of the radiopharmaceuticals
are used for medical diagnosis, while the rest are used for therapeutic purposes ([5], [6]).
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1.1.3 Molybdenum-99/Technetium-99m: The Most Common Radioisotope
The most commonly used radioisotope in diagnostic nuclear medicine is Tc-99m,
which is produced directly from the radioactive decay of Mo-99 ([5], [7]). Tc-99m is used
in approximately 30 million procedures per year, accounting for 80% of all nuclear
medicine procedures worldwide [2].
Mo-99 and Tc-99m do not exist naturally. Mo-99 is most commonly and
effectively generated by the fission of U-235 in nuclear reactors with a fission yield of
6.1% [3]. The reaction shown in Eq. (1.1) corresponds to the production of Mo-99 from
the fission of U-235, which occurs for approximately 6.1% of all fission reactions.
nSnMonU 4133
50
99
42
235
92 (1.1)
Mo-99 is formed from the nuclear fission of U-235 and consequently exists as a
fission by-product in uranium targets. These targets are specifically irradiated for
radioisotope production in nuclear reactors. The Mo-99 is then extracted in dedicated
processing facilities and placed in generators that are sent to various medical
institutions around the globe.
1.2 Demand for Molybdenum-99
Every week, approximately 300 therapeutic doses of medical isotopes and 30000
diagnostic treatments are performed in Canadian hospitals [2]. Over 10000 hospitals
worldwide use radioisotopes of which 90% are used strictly for diagnosis [4].
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In developed countries, which account for 26% of the world population, the
relative use of diagnostic nuclear medicine among all health procedures is 1.9% per year,
one tenth of which involves therapy using radiopharmaceuticals [4]. In the United
States, there are approximately 18 million nuclear medicine procedures per year
(population of 311 million), and there are about 10 million procedures performed in
Europe (population of 500 million). In Australia, there are approximately 560000
procedures performed per year (population of 21 million) out of which 470000 of these
procedures are done using reactor produced isotopes [4].
In North America, the demand for Mo-99 ranges from 5000 to 7000 six-day
Curies per week with an estimated annual growth rate between 3 and 5% [8]. Canada
accounts for approximately 1/11 of the total North American consumption. A
breakdown of the global demand of Mo-99 in 2009 is shown in Figure 1-1.
Curie is the unit of radioactivity (1 Curie = 3.7x1010 disintegrations per second or
Becquerels, Bq). A six-day Curie is a unit of measure most commonly used in the industry
which equates to the amount of Mo-99 remaining in a Tc-99m generator six days after
shipment from the producer’s facility. In other words, the producers usually calibrate a
shipment value to the activity of the Mo-99 isotopes 6 days after it leaves the production
facility [8].
The worldwide demand for Mo-99 has reached approximately 12000 six-day
Curies per week [7]. When accounting for the processing time and efficiency, 12000 six-
day Curies is equivalent to about 77000 end-of-bombardment Curies which is 160 mg of
Mo-99 at the end of the irradiation stage [8]. The demand for medical isotopes for
Page | 7
diagnosis and therapy purposes is expected to grow over 10% per year worldwide ([4],
[9]).
Figure 1-1: Approximate Global Demand for Molybdenum-992
1.3 The Big Five Medical Isotope Producing Reactors
Currently, five nuclear reactors are producing approximately 95% of the world’s
supply of Mo-99 [11]. The five are the Chalk River National Research Universal (NRU)
reactor in Canada, the High Flux Reactor (HFR) in the Netherlands, BR2 in Belgium,
OSIRIS in France, and the SAFARI-1 in South Africa. In addition to the production of
2 Data taken from Reference [10]
44%
22%
14%
4%
16%
United States Europe Japan Canada Other
Page | 8
medical isotopes, these reactors also provide multiple services such as nuclear fuel
testing and material research.
These big five industrial scale research reactors producing most of the world’s
Mo-99 supply are government-owned and funded. The global market share of these five
major isotope producing reactors is shown in Table 1-1. The Canadian NRU reactor and
the HFR in Netherlands, each produce approximately 30% to 40% of the global demand
for Mo-99. The other two European reactors and the reactor in South Africa combined,
produce approximately 36% of the Mo-99 supply. The smaller reactors around the
world support approximately 4% of the world’s demand of Mo-99.
As of 2014, Canada’s NRU in Chalk River is 57 years old, HFR in Petten,
Netherlands is 53 years old, SAFARI-1 in Pelindaba, South Africa is 49 years old, BR-2 in
Mol, Belgium is 53 years old, and OSIRIS in Saclay, France is 48 years of age [12].
Table 1-1 also provides additional information on these five reactors (e.g., thermal
powers and neutron fluxes, and estimated reactor stop date).
The majority of the smaller Mo-99 producing reactors around the globe
accommodate local or regional medical isotope markets. Some regional producers of
Mo-99 are Australia, Argentina, Germany, Indonesia, and Poland as shown in Table 1-2.
The research reactors in the aforementioned countries do not produce the commercial
quantities necessary to compensate for the closure of one or more of the big five reactors.
However, they can act as a short term make-up when one of the big five reactors
experiences an outage. The regional reactors are listed in Table 1-2.
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Table 1-1: Worldwide Production Capacity of Molybdenum-99 ([11], [12],
[13], [14])
Reactor Approximate Market Share (%)
Thermal Power (MW)
Thermal Neutron Flux (n·cm-2·s-1)
Target Type
Estimated Stop Date
National Research Universal (NRU) (Canada)
30% to 40% 135 4x1014 HEU 2016
High Flux Reactor (HFR) (Netherlands)
30% to 40% 45 2.7x1014 HEU 2022
SAFARI-1 (South Africa)
15% 20 2.4x1014 HEU 2025
BR2 (Belgium) 14% 100 1x1015 HEU 2026 OSIRIS (France) 7% 70 1.7x1014 HEU 2018 Rest of the world
4% - - -
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Table 1-2: Small-Scale Producers of Molybdenum-99 in 2011 ([8], [11], [14])
Reactor Typical Capacity (Six-day Curies)
Thermal Power (MW)
Thermal Neutron Flux (n·cm-2·s-1)
Target Type
OPAL (Australia) 20 3x1014 LEU
RA-3 (Argentina) 200 5 4.8x1013 LEU MARIA (Poland) 30 3.5x1014 HEU LWR-15 (Czech Republic)
10 1.5x1014 HEU
WWR-TS (Russia) 15 1.8x1014 HEU IRT-T (Russia) 6 1.4x1014 HEU FRM-II (Germany) 20 8x1014 HEU ETTR-2 (Egypt) 250 22 2.8x1014 LEU RSG-GAS (Indonesia)
150 30 2.5x1014 HEU
PARR-1 (Pakistan)
20 10 1.7x1014 HEU
RECH-1 (Chile) 250 5 7x1013 LEU
Page | 11
1.4 Introduction to Radioisotope Production in Nuclear Reactors
Neutrons in nuclear reactors drive the nuclear reactions that must take place for
the successful production of various radioisotopes. The neutron flux typically achieved
in nuclear reactors is several orders of magnitude higher when compared to neutron
generators and other isotopic neutron sources [7], for example ~1014 n·cm-2·s-1 for a
typical nuclear reactor versus 1010 n·cm-2·s-1 for a typical neutron source. The quantity
and activity of radioisotopes is directly proportional to the neutron flux. This explains
why nuclear reactors that have high neutron flux values hold a strategic advantage in the
production of medical radioisotopes.
Although all reactors are neutron sources; not all are suitable for Mo-99
production. The factors that determine whether a reactor is suitable for Mo-99
production are:
(i) neutron flux available for target irradiation,
(ii) volume of the irradiation rigs into which targets can be placed, and
(iii) in the case where targets are fissionable isotopes of enriched uranium, a further
consideration is heat removal from the targets [15].
Currently, nuclear reactors are producing Mo-99 and its decay product Tc-99m
through irradiation of HEU targets. After spending several days in the reactors, these
irradiated targets are sent for processing to dedicated processing facilities [7].
Page | 12
1.5 Alternative Methods for Producing Molybdenum-99
A nuclear reactor is not a requirement when it comes to producing Mo-99. An
accelerator can also be utilized to generate Mo-99 by photo-fission of the U-238 atoms
present in NU. Alternative options for the production of Mo-99 include eliminating
uranium from the process by using other isotopes of molybdenum and converting them
to Mo-99. This consists of four possible reactions: 98Mo(n,γ)99Mo (neutron activation)
occurring inside a reactor, 100Mo(γ,n)99Mo, 100Mo(p,pn)99Mo and 100Mo(p,2n)99mTc
(neutron emission) using accelerators.
1.5.1 Photo-fission Process 238U(γ,f)99Mo
In this method, a high intensity beam of photons is generated and directed at
U-238 [16]. This reaction results in nearly the same 6.1% fission yield for Mo-99 as the
fission yield of U-235 in nuclear reactors. The cross-section for this reaction is about
1000 times smaller than the neutron fission cross-section of U-235. As a result, a
relatively large number of accelerators would be required to produce significant
amounts of Mo-99. One estimate is that half a dozen accelerators are needed to supply
30% to 50% of North American demand [8].
1.5.2 Neutron Activation of Molybdenum-98
The reaction, 98Mo(n,γ)99Mo (neutron activation), requires thermal (~ 0.025 eV)
or epithermal (0.025 – 1.0 eV) neutrons. However, only a small portion of this target is
converted to Mo-99 because the cross-section of this reaction is small (σthermal ~ 0.14
barns). In addition, although neutron activation of molybdenum generates the desired
Page | 13
radionuclide with little to no waste stream, Mo-99 produced through this method is not
“carrier-free” as it contains Mo-98 (natural molybdenum contains approximately 24%
of Mo-98) which is chemically identical to Mo-99 and behaves as a contaminant.
The Mo-99 produced through neutron activation has low specific activity and
requires a large number of targets to produce significant quantities of Mo-99. A nuclear
reactor would still be required to provide the necessary neutron flux for this method.
Furthermore, the potential exists for increased elution of undesirable Mo-98 when
formulating patient dosages [8].
1.5.3 Neutron Emission from Molybdenum-100
The three neutron emission methods (100Mo(p,pn)99Mo, 100Mo(γ,n)99Mo and
100Mo(p,2n)99mTc) require accelerators that can generate very high intensity beams of
protons (500 μA) or electrons, in order to create photons powerful enough to overcome
the significantly smaller cross-sections for these reactions.
When the 100Mo(γ,n)99Mo reaction is used, high energy photons known as
Bremsstrahlung radiation are produced by the electron beam as it interacts and loses
energy in the ‘converter’ target. The photons are subsequently used to irradiate another
target material (Mo-100) placed just behind the converter to produce Mo-99 via neutron
emission.
The 100Mo(p,2n)99mTc neutron emission method, results in the direct production
of Tc-99m which has a significant disadvantage due to its short half-life. It is not an ideal
method to produce Tc-99m because any need to ship the Tc-99m generators over
Page | 14
distances would reduce the usefulness to the end-user and by extension, to the patient
[8].
1.6 Radioactive Decay of Molybdenum-99/Technetium-99m
Mo-99 decays into Tc-99m, which is then extracted from the generators and
combined with other reagents to form a radiopharmaceutical that can be given to
patients. Tc-99m is an ideal radioisotope for diagnostic nuclear medicine ([7], [10], [17])
because of its physical and chemical properties. The 6.01-hour half-life of Tc-99m is
neither too long nor too short for a medical procedure. Its parent radionuclide, Mo-99,
has a 66-hour half-life which provides sufficient time for processing and long-distance
transportation, and thus permits shipping under the form of a Mo-99/Tc-99m generator
[5].
Conversely, due to its short half-life, Tc-99m cannot be stockpiled or produced
directly in nuclear reactors or through neutron activation as a final product, nor can it
be shipped to hospitals and radiation clinics around the globe. Instead, Tc-99m is
obtained through elution with a sterile saline solution from an alumina column
containing its parent isotope Mo-99. The alumina column assembly is known as a
Tc-99m ‘generator’ [3].
Another desirable property of Tc-99m, is the energy of the emitted gamma
radiation, which is in a range that allows a clear image to be produced in a gamma
camera. In addition, since 89% of Tc-99m emits pure gamma radiation that is energetic
Page | 15
enough to pass through human body without significant attenuation, this keeps the total
dose administered to patients low ([1], [18]).
Figure 1-2 shows the decay sequences of Mo-99 to Tc-99 with the respective half-
lives and yields. Mo-99 disintegrates with a half-life of 66 hours to either Tc-99m or
Tc-99 by emitting a beta particle. The “m” in Tc-99m stands for ‘meta-stable’. The
Tc-99m radionuclide is unusual since it undergoes a gamma decay into Tc-99 ground
state rather than decaying instantaneously, as is the case with most excited
radionuclides produced through β- or β+ decay [19]. As depicted in Figure 1-2, Tc-99m
decays by isomeric transition. The principal gamma-emission associated with the
transition from the meta-stable state to the ground state of Tc-99 emits a 140-keV
photon [5]. Using a scintillator that is made up of special plastic or NaI-Tl crystals, the
photon is captured by the detector, and converted into visible light photons which are
then converted by a photomultiplier tube into electrical pulses and counted
electronically [20].
Page | 16
Figure 1-2: Principal Decay Scheme of Molybdenum-993
1.7 Considerations in the Production of Molybdenum-99 in Nuclear
Reactors
The activity of Mo-99 produced in a target is a function of irradiation time, the
thermal neutron fission cross-section for U-235, the thermal neutron flux induced on the
target, the mass of U-235 in the target, and the half-life of Mo-99 [22]. For a typical
reactor with thermal neutron fluxes on the order of 1014 n·cm-2·s-1, irradiation times of
about 15 to 20 days are sufficient to achieve the maximum possible activity of Mo-99 in
the targets. Beyond this equilibrium stage, the amount of Mo-99 produced in the targets
3 Reproduced from Reference [21]
Page | 17
approximately balances the amount of Mo-99 being lost to radioactive decay [8].
Additional irradiation time is also uneconomical due to the fact that there would be
additional accumulation of other undesirable fission products, adding to the radioactive
fields from the targets, and the wastes that ultimately require disposal.
In theory, for a target irradiated by a thermal neutron flux inside a reactor, the
rate of production can be represented by the following mathematical relationship:
NNdt
dNT (1.2)
For Mo-99 production in U-235 targets, Eq. (1.2) can be solved to determine the
specific activity of radioactive atoms at time ‘t’:
)/()1(6.0 99
gBqeA
fS tfMo
(1.3)
In Eqs. (1.2) and (1.3), NT is the total number of U-235 atoms in the target, N is
the number of Mo-99 atoms produced as a fission product, 99Mof is the fraction of fission
products leading to the production of Mo-99 (6.1%), f is the microscopic fission cross-
section, is the thermal neutron flux, and is the Mo-99 decay constant. Figure 1-3
illustrates the buildup of Mo-99 activity for a target irradiated in a thermal neutron flux
of approximately 2×1014 n·cm-2·s-1, which is typical of a CANDU reactor.
Page | 18
Figure 1-3: Buildup of Molybdenum-99 Radioactivity for a Neutron Flux
Typical of a CANDU-6
1.7.1 Molybdenum-99 Target Processing Techniques
After irradiation in the reactor for several days, the HEU or LEU target is
chemically processed by one of the two processes:
i) acid dissolution and molybdenum separation process (Cintichem process), or
ii) alkaline dissolution process.
The acid dissolution was developed by Cintichem Incorporated. The technology
was later purchased by the US Department of Energy (DOE) following the
decommissioning of Cintichem’s Tuxedo, NY reactor. The facility is currently focused on
proposing modifications to convert to an LEU target for US supplies of medical isotopes.
0.00E+00
2.00E+12
4.00E+12
6.00E+12
8.00E+12
1.00E+13
1.20E+13
1.40E+13
1.60E+13
1.80E+13
2.00E+13
0 100 200 300 400 500 600 700
Spe
cifi
c A
ctiv
ity
of
Mo
-99
(B
q/g
)
Time (Hours)
Page | 19
A proprietary Nordion Incorporated acid-dissolution process is currently used
for the isotope production from NRU. The process is believed to be very similar to the
Cintichem process according to available sources [20]. A brief overview of the acid
dissolution process is provided below.
The alkaline dissolution process is generally used for targets that contain
aluminum and is currently being used by all major isotope producers except Nordion
Incorporated (formerly known as MDS Nordion).
Following several days of irradiation, the targets are removed and allowed to cool
in water for up to half a day. The targets are then transferred to an associated “hot cell”
facility. The hot cells are cabins which are shielded by lead and concrete, and are able to
withstand the decay heat and intense radiation fields of the targets. The time it takes for
the processing of the targets in the hot cells is optimized in order to minimize Mo-99
losses due to radioactive decay. Approximately 1% of the generated Mo-99 is lost to
decay per hour after end-of-bombardment inside a nuclear reactor [23]. The processing
time required following irradiation inside a reactor means that a significant amount of
Tc-99m will eventually be lost.
In the hot cell facility, the cladding is punctured and volatile fission products such
as Kr-85 and Xe-133 are removed. The target assembly is dissolved in hot nitric acid,
forming a nitrate solution containing uranium, molybdenum, and other fission by-
products. The solution is poured through an alumina (Al2O3) column that adsorbs the
nitrates. The column is then washed with additional nitric acid to elute excess uranium
and other fission by-products, leaving the molybdenum bounded within the column
Page | 20
matrix. Sodium hydroxide is then added to the column which elutes purified Mo-99 [5].
This process typically yields recovery greater than 85-90% of the Mo-99 in the targets
[8].
The removed Mo-99 is immediately shipped to Covidien in Mansfield,
Massachusetts or Lantheus Medical Imaging in North Billerica, Massachusetts, where
they manufacture Tc-99m generators. These Tc-99m generators are used to extract the
decayed daughter Tc-99m isotopes from the parent Mo-99. Finally, the generators are
then shipped to destinations around the globe as depicted in Figure 1-4.
Figure 1-4: Global Supply Chain of Molybdenum-99 and Utilization
Schematics4
4 Reproduced from Reference [12]
Page | 21
1.7.2 Technetium-99m Generators
Manufacturing of a Tc-99m generator generally consists of adsorption of Mo-99
onto an alumina column. Positively charged beads are used in the alumina column to
adsorb the Mo-99 as Mo99O42- [17]. When the Mo-99 decays it forms pertechnetate TcO4-.
Due to its single charge, pertechnetate is less tightly bound to the alumina. The column
has a higher affinity for the Mo-99 than the Tc-99m ensuring the preferential elution of
Tc-99m when a saline solution is poured through the column. Breakthrough of small
quantities of Mo-99 still occurs. The amount of breakthrough is one of the quality control
parameters for manufacturing Tc-99m generators and is regularly monitored [17].
Due to the short half-life of Mo-99 (66 hour), the complete manufacturing process
must take place quickly. For this reason, most nuclear medicine institutions rely on
weekly shipments of Tc-99m generators to meet their demands. The supply chain is
currently capable of supplying Tc-99m from reactor extraction to the patient in less than
48 hours in an ideal case.
When the supply reaches the hospital or the radiation clinic, a radiopharmacist
calculates the amount of Tc-99m generated by disintegration of Mo-99 nuclides based
on the transient equilibrium that exists between the two nuclides. For commercial kits
such as Cardiolite®, the Tc-99m is eluted from the column with sterile saline (0.9%
NaCl), as sodium pertechnetate (Na99mTcO4), and is then mixed with other reagents into
a final form that can be administered to patients. The column is re-used, or “milked”,
until most of the Mo-99 has decayed and the column is exhausted [5]. Figure 1-5 shows
the “milking” process of Tc-99m from its first elution.
Page | 22
TechneLite® is a Tc-99m generator that is produced by Lantheus Medical Imaging
Incorporated. Dosage from TechneLite can range from 0.08 mCi/kg for pediatric thyroid
imaging to 0.28 mCi/kg for blood pool imaging of the heart [24]. Cardiolite® is another
Tc-99m generator produced by Lantheus Medical Imaging that is widely used in cardiac
stress test applications.
Figure 1-5: Decay of Molybdenum-99 and Buildup of Technetium-99m Activity
after Each Elution, Calculated for 7 Days5
5 Reproduced from Reference [17]
Page | 23
1.7.3 Spent Fuel Considerations
It is important to consider various concerns that generally arise in the production
of Mo-99 from the perspective of waste management. Management of waste starts from
the planning, designing and construction phase of the Mo-99 production facility and
continues through the operational phase. Waste management strategy has to also
account for the route taken by the spent targets and long-lived fission products.
Establishment and implementation of an effective and safe waste management strategy
is generally a licensing requirement which is approved and regulated by the authorities.
Target fabrication, irradiation, and extraction of Mo-99 from targets generate
significant quantities of chemical and radioactive waste. Waste is generated as solids,
liquids, and gases, and can include material in the low, intermediate and highly
radioactive waste categories [25]. Initial treatment of waste streams is usually done at
the production site, from where it is transferred to short or long term storage facilities.
Treatment of gaseous waste is generally carried out in the production facility on site
while treatment of solid and liquid radioactive waste can be performed off-site [25].
Figure 1-6 is a generic flow chart of waste streams generated from Mo-99 production.
The conversion from HEU to LEU targets, which is underway at most of the
current Mo-99 producing facilities, would generate even larger quantities of waste. If
current target dissolution processes are maintained, the existing waste storage facilities
may not be able to accommodate a five-fold estimated increase in waste products.
Page | 24
A study conducted by the Nuclear Energy Agency gives an insight on the
increased waste levels that are to be expected with LEU-based targets [26]. For example,
the annual amount of waste corresponding to the 12000 six-day Curies per week
production rate were 215 kg LEU uranium waste vs. 43 kg of HEU waste and 25 g of
Pu-239 for LEU vs. 1.2 g for HEU. These numbers are estimated annually for 20%
enriched targets vs. 93% enriched targets, respectively. It is further noted from the OPAL
reactor in Australia, LEU processed targets will yield increased volumes of intermediate
and low-level liquid waste in comparison to HEU strategies [26]. However, the
possibility remains that by converting liquid waste products to its solid form will
optimize waste storage tanks that are currently operating below capacity and hence,
waste storage will not be significantly impacted [8].
Page | 25
Figure 1-6: Generic Flow Chart of Waste Streams Generated from
Molybdenum-99 Production6
6 Adapted from Reference [27]
Page | 26
1.8 CANDU Reactors and The DRAGON Lattice Code
1.8.1 Using CANDU Reactors for Molybdenum-99 Production
CANDU reactors are known as pressurized heavy water reactors. The acronym
‘CANada Deuterium Uranium’ (CANDU) comes from the reactor’s use of heavy water as
a moderator and NU as fuel. The moderator fills a large tank called the calandria. The
calandria is penetrated by hundreds of horizontal fuel channels, each consisting of an
inner pressure tubes which contains natural uranium oxide fuel in a form of fuel bundles
and an outer calandria tube. The fuel is cooled by heavy water under high pressure. The
pressure channel design makes it possible to refuel the reactor continuously without
shutting it down. This is done by connecting in-tandem both sides of an individual
channel to a fuelling machine and a fuelling machine cooling circuit. Table 1-3 gives a
breakdown of the CANDU reactors and CANDU-derivatives that exist around the world.
Figure 1-7 depicts the important components of a typical CANDU reactor. A
typical CANDU fuel channel is shown in Figure 1-8. The diagram shows the channel
inlet/outlet end fitting and the arrangement of the fuel bundles in the pressure tube.
Page | 27
Table 1-3: Status of CANDU reactors and CANDU-Derivatives in 2014 ([28],
[29])
Country No. of Reactors
Status Capacity (MWe net)
Argentina 3 Operational 1627 Canada 19
6 Operational Permanent Shutdown
13500 2143
China 2 Operational 1300 India 18
4 Operational Under Construction
4091 2520
Republic of Korea
4 Operational 2684
Pakistan 1 Operational 90 Romania 2 Operational 1300
Page | 28
Figure 1-7: CANDU Reactor Face7
7 Reproduced from the CANTEACH website [30]
Page | 29
Figure 1-8: A Typical CANDU Fuel Channel8
8 Reproduced from the CANTEACH website [31]
Page | 30
1.8.2 The DRAGON Code
Analysis of the proposed bundle designs is performed at the lattice level using the
lattice transport code DRAGON version 3.05 [32], [33], [34]. DRAGON has been
developed at École Polytechnique9 de Montreal and is considered one of the
recommended codes by the nuclear industry to perform lattice calculations. The code
solves the integral neutron transport equation using 2-D and 3-D collision probability
techniques.
DRAGON is a lattice code which is used to solve the neutron transport equation
for a given geometry. DRAGON includes all of the functions that characterize a lattice
cell code divided into several calculation modules. The modules are linked together by
GAN generalized driver. The exchange of information is ensured by well-defined data
structures. This is done so that new calculation techniques can be implemented in the
code [35].
DRAGON consists of two main components, one -group collision probability
tracking modules and multigroup flux solvers. The interface-current technique is used
by the JPM tracking option at the level of each homogenous region associated with a
9 The École Polytechnique de Montréal is an engineering school/faculty affiliated with the
University of Montreal in Montreal, Quebec, Canada.
Page | 31
specific geometry. In cases where a multiplicative medium is analyzed, DRAGON
performs power iterations to find the effective multiplication factor.
The effective multiplication factor (keff) is defined as the ratio of the number of
fissions (or fission neutrons) in one generation divided by the number of fissions (or
fission neutrons) in the preceding generation. keff provides an idea of deviation of the
system from equilibrium. The system can be termed critical (the production and
destruction rates are equal), subcritical (the production rate is smaller than destruction
rate) or supercritical (the production rate is greater than destruction rate) based on the
following definition:
𝑘𝑒𝑓𝑓 {< 1 𝑟𝑒𝑎𝑐𝑡𝑜𝑟 𝑠𝑢𝑏𝑐𝑟𝑖𝑡𝑖𝑐𝑎𝑙 = 1 𝑟𝑒𝑎𝑐𝑡𝑜𝑟𝑐𝑟𝑖𝑐𝑡𝑖𝑐𝑎𝑙 > 1 𝑟𝑒𝑎𝑐𝑡𝑜𝑟 𝑠𝑢𝑝𝑒𝑟𝑐𝑟𝑖𝑡𝑖𝑐𝑎𝑙
(1.4)
The multiplication factor of an infinite lattice calculation is represented as kinf. In
the case where the coefficient of reflection at the surface boundary is set to 1
everywhere, as is the case with the models analyzed in this thesis, the outgoing fluxes
will be reflected back into the volume, making the neutron leakage equal to zero, and
thus making keff equal to kinf. It is referred to as the reflective boundary condition.
Another important quantity in reactor neutronics is known as reactivity (ρ). It is
defined as the fractional departure of a system from criticality and is calculated as:
eff
eff
k
k 1 (1.5)
Page | 32
The system reactivity change can be positive or negative depending on the
process involved. For example, addition of any form of poison, like boron in the
moderator or insertion of control rods, brings about a reduction in reactivity, while
removal of poison or addition of fresh fuel or enrichment of NU can bring about an
increase in reactivity.
In the present study, the focus is on change in reactivity from introducing a region
of enriched fuel by comparing it to that of NU. The change in reactivity ∆ρ, introduced
due to enrichment can be defined as:
mkxkk enriched
eff
natrual
eff
100011
(1.6)
There are microscopic cross-section libraries that are structured according to a
standard format and are accessible to DRAGON [34]. The output data stream provided
by DRAGON is the source for obtaining useful information such as macroscopic cross-
section, neutron fluxes, etc.
Page | 33
Chapter 2
Production of Molybdenum-99 in Nuclear Reactors: Present
and Future
Mo-99 is obtained from the fission of U-235, and is principally produced through
the 235U (n,f) 99Mo 99mTc reaction using the five government-owned and funded multi-
purpose reactors listed in Table 1-1. The ageing of these five research reactors has
required ever growing shutdown periods for maintenance and repair. This has made the
supply of Mo-99 more fragile and a topic of concern for the medical community.
Additional challenges are cast on the supply of Mo-99 due to the fact that the
major Mo-99 manufacturers have been using HEU (~93%) for target material, except for
SAFARI-1 in South Africa that uses 45% [8]. Some of the regional producers of Mo-99
are using LEU targets, including for example, the RA-3 reactor in Argentina and the OPAL
reactor in Australia [8].
The challenges arising from the limited number of ageing reactors and the use of
HEU, which ultimately affect the reliable supply of Mo-99 worldwide, will be explored
further in this Chapter.
Page | 34
2.1 Current Molybdenum-99 Supply Challenges
Five nuclear research reactors are producing most of the worldwide supply of
Mo-99 as listed in Table 1-1. In 2007, major disruptions occurred in the global supply of
Mo-99 due to an extended shutdown of the NRU reactor. The disruptions lasted for
several weeks. As a result, many of the diagnostic testing and procedures for life-
threatening conditions were cancelled affecting tens of thousands of patients throughout
Canada and the US [2].
The crisis began when the NRU reactor did not return to operation for several
weeks following a routine maintenance shutdown due to regulatory issues. The NRU
shutdown event was followed by an extension of the planned outage at HFR-Petten due
to leaks, and an unplanned shutdown of an isotope processing facility due to Iodine-131
release from the waste stream [12]. Concerns over the long term supply of medical
isotopes were further exacerbated by the government of Canada’s decision to stop the
development of the MAPLE reactors. These reactors were being designed and built to
meet the world’s demand of medical isotopes, specifically Mo-99, I-125, I-131, and
Xe-133 [36]. There are currently no reliable long-term substitutes to NRU to ensure
continuity in the supply of Mo-99 to the world.
Page | 35
2.2 Conversion of Molybdenum-99 Targets from Highly-Enriched
Uranium to Low-Enriched Uranium
The current producers of Mo-99 use HEU targets of ~93 wt% U-235 with the
exception of SAFARI-1 reactor in South Africa which uses 45 wt% U-235 targets. For the
NRU reactor, HEU from Y-12 National Security Complex in Oak Ridge, Tennessee is
shipped to Chalk River Laboratories in Chalk River, Canada to be manufactured into
Mo-99 targets. Published records by the United States Nuclear Regulatory Commission
(US-NRC) report shipments of 10-25 kg of HEU per year from the US to Canada for Mo-99
production ([20]).
The most pressing change in the medical isotopes industry has been surrounding
the efforts to convert the fuel and the Mo-99 targets to LEU (less than 20% U-235 by
weight). In the interest of nuclear security and non-proliferation, many countries
around the world are making strides in the efforts to migrate from using HEU to LEU.
The movement was supported by the US House of Representatives in November of 2009
in the form of passing a legislation which would eliminate the US export of HEU for
isotope production in Canada within a period of 7 to 10 years [37].
Substituting LEU directly in place of HEU targets would reduce the Mo-99 yield
to approximately 20% of that generated from the HEU due to reduced number of U-235
atoms available for fission. The lower yield can be overcome by irradiating five times
more targets in the reactor, however the available reactor space limitations may
preclude such an option.
Page | 36
Irradiating five times more targets will also result in five times the volume of
separation waste leading to storage and disposal issues. In addition, employing LEU
targets will also increase the generation of fissile plutonium-239 due to neutron capture
by the higher proportion of uranium-238 atoms. However, plutonium can be ultimately
used to make mixed-oxide fuel for nuclear power plants as it is generally insoluble and
can therefore be separated from liquid wastes during processing of the LEU targets [8].
Research is underway to yield more efficient LEU target designs. Researchers are
looking at ways to alter the composition of LEU targets for the purpose of increasing the
density of U-235 in the targets [8]. The Reduced Enrichment for Research and Test
Reactors program was first established in 1978 at the Argonne National Laboratory by
the US Department of Energy. The primary objective of this program was to develop the
technology needed to use LEU instead of HEU in the research and test reactors, without
impacting the experimental performance, economics, or safety of the reactors [38].
There will have to be substantial economic incentives for any large producer of
Mo-99 to change from using HEU. Large investments would be required for
infrastructure, approval of new processes and procedures and the required research.
Any new process would need to be qualified by the various regulators, which is a long
and expensive process, adding to its cost. Implications regarding waste management
with respect to treatment of irradiated targets and disposal should also receive high
priority [39].
Page | 37
2.3 New Producers of Molybdenum-99 Worldwide
The current fleet of Mo-99 producers consisting of the big-five reactors is aging
and is expected to stop the production of Mo-99 in the next decade. The NRU is
scheduled for shutdown and to cease all production in the year 2016. The OSIRIS reactor
is expected to shut down by the end of 2018. These two reactors account for over a
quarter of the available capacity of Mo-99. This will drastically reduce the supply of
Mo-99.
Since the 2007 disruptions in the supply of Mo-99, several countries have
expressed interest in building modern research reactors dedicated to Mo-99 production
in order to curtail reliance on other countries for medical isotopes and to develop
domestic production capabilities. Some countries have proposed new projects to initiate
molybdenum production from an existing facility not originally built for that purpose.
Commissioning a new reactor for isotope production is a lengthy process. According to
a European Commission study on the supply of medical isotopes, it can take ten or more
years for any new project from the planning phase to become operational. If an existing
facility is upgraded to supply Mo-99, these facilities can take five or more years to
become operational depending on available equipment and facilities at the specific
reactor site [7].
Appendix A provides a list of potential producers that have the technological
resources to develop Mo-99 production capabilities. A general underlying objective of
these new initiatives is to develop domestic capabilities of producing Mo-99 and
reducing the dependence on foreign suppliers. In few cases where potential exists to
Page | 38
irradiate a large number of targets, exports of medical isotopes may occur from those
facilities to aid in meeting the global demand for medical isotopes.
2.4 Molybdenum-99 Production in Power Reactors
Production of Mo-99 using commercial power reactors is a novel idea considering
power plants are not normally used to produce radioisotopes. Other radioisotopes have
been produced using power reactors, particularly in CANDU reactors. In Canada, tritium
is recovered from the heavy water coolant [28]. The adjustor rods used in CANDU
reactors are also processed to produce cobalt-60 sources for industrial radiation
processing. However, most commercial power reactors generally restrict their use
solely to the generation of electricity.
The production of medical isotopes in power reactors involves several
interrelated areas such as target fabrication, neutronic analysis, thermalhydraulic
calculations, safety analysis, fuelling schemes, processing and transportation of
irradiated targets [28]. Another important factor is the number and volume of targets
being irradiated at a time, which will determine the yield of radioisotopes. Irradiation
time in reactor is another important factor in obtaining high specific activity.
The CANDU reactors and CANDU-derivatives have a pressure tube design that
permits these reactors to be refuelled online by connecting in-tandem to a fueling
machine. From the standpoint of Mo-99, a case can be made that irradiation of targets
Page | 39
in power reactors is similar to their irradiation in a research reactor in the sense that
these targets can be recovered at any time.
It is also possible to irradiate targets in the irradiation channels that exist in some
pressure tube type reactors ([26], 28]). Instrumentation channels can also be used to
irradiate targets in most reactors. However, this may be a challenging task requiring
reconfiguration of the reactor instrument calibration and possibly the core neutronics.
Irradiation of uranium targets in CANDU has already been proposed in recent
past ([22], [40], [41]). Researchers at McMaster University have analyzed a new 37-
element fuel bundle containing a combination of slightly enriched/depleted uranium
pins that, when irradiated in a CANDU reactor, could yield 100% to 120% of the world
demand of Mo-99 ([22], [40]). The researchers have proposed modifications to the 37-
element fuel bundle that would contain 1.5% to 3% enriched uranium oxide fuel either
in the second and third ring, or in the fourth ring of the fuel bundle, with the rest of fuel
pins containing depleted uranium. Calculations done in the WIMS-AECL-v3.121 lattice
code showed that these targets, when irradiated in the central and periphery channels,
produced significant amounts of Mo-99 without adversely affecting important reactor
safety parameters such as neutronics, heat rating limits, and including any significant
impact on standard fuelling operations. However, the design constraints used in the
McMaster research had wide margins allowing for the Mo-99 producing bundle
neutronics to deviate significantly from the reference value. For example, a reactivity
difference of 10 to 15 mk from the reference CANDU bundle was deemed acceptable for
Page | 40
the Mo-99 producing bundles, potentially leaving a gap in the safety analysis and a need
for confirmation of the design using full core calculations and experimental testing.
Page | 41
Chapter 3
Methodology for the Development of a Molybdenum-99
Producing 37-Element Fuel Bundle Design
3.1 Design Objectives
One of the attractive features of the CANDU reactor is its versatility in fuelling
applications. Opportunity exists for evolutionary improvements in the CANDU fuel
design that can produce large quantities of medical isotopes while maintaining its power
production targets. The ability to refuel online while maintaining a good thermal
neutron economy in the core makes CANDU reactors a strong candidate for producing
significant quantities of Mo-99 to meet the global demand of medical isotopes. On-power
fuelling of the CANDU reactors allows the gradual introduction of new fuel bundle
designs intended for Mo-99 production.
The objective of this thesis is the development of new 37-element fuel bundles
that, when irradiated in a standard CANDU reactor, are able to produce significant
quantities of Mo-99, and which have neutronic and thermalhydraulic properties nearly
identical to those of the standard CANDU fuel bundle. This objective translates into six
design requirements:
1. The bundle shall use LEU fuel of less than 20% U-235 enrichment by
weight and produce Mo-99 in sufficient concentrations to be extracted
using chemical processes currently in use.
Page | 42
2. The hydraulic resistance of the Mo-99-producing bundle shall be identical
to that of a standard CANDU fuel bundle.
3. The bundle shall be dimensionally compatible with the fuel channel
components and with the appropriate fuel handling components.
4. The reactivity of the Mo-99-producing bundle shall be close to that of a
standard CANDU fuel bundle. A reactivity change of ±1 mk of standard
CANDU is deemed acceptable.
5. The power generation rate in the Mo-99-producing bundle shall be similar
to that of the standard CANDU fuel bundle when placed in the same
position in the core.
6. The bundle shall demonstrate that the operating and safety margins
regarding fuel sheath dryout power and fuel centreline temperatures are
maintained with the use of the new bundles in the core.
3.2 Design Plan and Strategy
The plan is to consider various design options that utilize the standard
37-element fuel bundle geometry. The proposed designs for Mo-99 production range
from a fuel bundle comprised of a combination of enriched and depleted UO2 concentric
fuel layers in the outer rings and NU in the centre and inner rings, to a fuel bundle with
mixed fuel pins (enriched + depleted uranium) in all four rings of the 37-element bundle
Page | 43
for maximum yield of Mo-99. Other design options include a fuel-bundle comprised of
uranium metal fuel, which is utilized to achieve higher margins for fuel centreline
melting (due to the metal’s higher thermal conductivity compared to the ceramic) and
ease of manufacturing with respect to the proposed thickness of the enriched fuel region.
Five different design options are assessed in this study. Designs 1, 2 and 3 use
mixed fuel targets (enriched + depleted) in Ring 4 and natural UO2 in the centre and inner
rings. Designs 4 and 5 use mixed fuel targets in all rings. Design 3 and 5 use uranium
metal fuel in the target pins as a test for improved safety margins with respect to fuel
centreline temperatures. A pictorial representation of the various designs options that
are considered in this study is shown in Figure 3-1.
As discussed in Chapter 2, nuclear proliferation concerns have limited the
enrichment in target bundles to 20 wt% of U-235. Due to the fact the ratio of Mo-99 yield
to the total fuel volume processed is low for NU, from the perspective of maximizing the
yields of Mo-99, use of higher enrichment is advantageous. Hence, use of 19.5 wt% of
U-235 enrichment, which is just below the HEU category, is recommended for this study.
The depleted uranium region is assumed to have 0.20% of U-235 by weight.
Depleted uranium is a by-product of the uranium enrichment process. Different fuel
enrichment facilities may have different end-cycle enrichment of uranium tails. Because
the enrichment of most uranium tails is typically less than 0.3% [42], 0.2 % is an easily
achievable value to be used as depleted uranium fuel in the proposed designs.
Page | 44
Figure 3-1: A Pictorial Representation of the Proposed Designs Assessed for
Molybdenum-99 Production10
10 The base image of the 37-elment bundle is adapted from Reference [43]
19.5% Enriched
UO2
0.2% Depleted
UO2
Natural UO2
19.5% Enriched
UO2
0.2% Depleted
UO2
Natural UO2
19.5% Enriched
U-Metal
0.2% Depleted
U-Metal
Natural UO2
19.5% Enriched
UO2
0.2% Depleted
UO2
19.5% Enriched
U-Metal
0.2% Depleted
U-Metal
Page | 45
3.2.1 Satisfying Design Requirements
In this section, the methodology that is adopted to satisfy the design
requirements listed in Section 3.1 is presented in detail.
Requirements 2 and 3:
The new fuel bundle design is based on the standard 37-element CANDU fuel
bundle. The bundle geometry is kept dimensionally identical to the standard CANDU
bundle. This allows the new design to have the same hydraulic resistance as the
reference bundle and, hence, be compatible with fuel channel components and the
appropriate fuel handling components in order to allow online refuelling.
Requirements 2 and 3 are thus satisfied.
Requirement 4:
Fuel pins in some (or all, depending on the specific design) rings are divided into
two concentric regions, one consisting of enriched uranium fuel and another consisting
of depleted uranium fuel. The relative dimension and position of the enriched-fuel and
depleted-fuel regions are determined from the condition that the bundle has a fresh fuel
infinite-lattice k-infinity (kinf) value that is similar to the standard CANDU fuel lattice
along with the condition on the fuel heating and centreline temperature limits. The cell
fresh fuel kinf is determined by the DRAGON code for the specified infinite lattice model
geometry. The kinf value needs to be as close as possible to the reference CANDU bundle
to allow for existing operational practices and bundle safety characteristics to be
maintained.
Page | 46
In order to meet the bundle reactivity criterion (Requirement 4), Task 1 has been
created and addressed further in Section 4.1.
Requirement 5:
Requirement 5 is implicit in the sense that a bundle with the same kinf as the
standard CANDU bundle and with identical overall bundle geometry will have average
two-group cross-sections similar to the standard CANDU bundle resulting in similar
power generation rates. Hence, Requirement 5 is also met by satisfying Requirements 2
and 4.
Task 1
Calculate the thickness (or radius) of enriched fuel region for the various
design options considered which yields a fresh fuel infinite-lattice kinf
value that is similar to that of the reference CANDU bundle. For this
study, a difference in reactivity (Δρ) value of ±1 mk compared to the
reference CANDU bundle is considered acceptable.
Page | 47
Requirement 6:
Fuel sheath dryout and fuel centreline temperatures are two phenomena that
serve as indicators of the onset of a heat transfer crisis and deteriorating bundle safety
characteristics. Heat generated in the fuel volume must be transported out through the
fuel surface.
The linear power rating represents the power produced per unit length (W/m)
of a fuel element. The linear heat rating of the element primarily dictates the sheath
temperature rise in case of a dryout. The heat flux is defined as the heat transferred per
unit surface area (W/m2). Generating excessive power from a bundle causes sheath
temperature to rise and bundle critical heat flux (CHF) and fuel centreline melting
margins to diminish. The CHF characteristics of a bundle are functions of bundle radial
flux distribution from ring-to-ring, bearing pad height, channel creep profile, fuel string
axial flux distribution. Other design features (such as end cap, end plate, etc.) also affect
CHF characteristics of a bundle.
Designs 1, 2 and 4 have the same fuel pellet and sheath diameters as the reference
CANDU bundle. This ensures the ability of the bundle to maintain the same
hydrodynamic properties as the reference CANDU bundle. For a bundle that is
dimensionally identical to the reference bundle with similar power generation rates, its
available margins to CHF can be determined by making a comparison of the linear power
ratings of the highest-power pins in both bundles.
Page | 48
Designs 3 and 5, which use uranium metal as fuel, have the same pin diameter,
but a smaller fuel pellet diameter. The increase in parasitic absorption due to the thicker
cladding is balanced by increasing the thickness of the enriched layer as part of the
activities performed under Task 1. Similar assertions regarding the CHF margins can be
made for Designs 3 and 5.
The second important safety parameter is fuel centreline temperature, which
must not exceed the values specified for the standard CANDU bundle for the same bundle
heat generation rates. The new fuel bundles will have non-homogenous fuel
composition containing concentric fuel regions inside Mo-99 target pins. Hence, meeting
the linear heat rating limits alone will not ensure adequate margins to the fuel centreline
melting.
The outermost ring (Ring 4) of the 37-element fuel bundle generally has the
highest linear heat rating value due to its proximity to the moderator and therefore to
the highest flux of thermalized neutrons. This is especially true if the outermost ring
contains a region of enriched fuel as is the case in the proposed designs (see Figure 3-1).
The enriched fuel region, due to its increased rate of fission and consequently higher
power density, creates the possibility of having a higher than reference centreline
temperature in the fuel.
To satisfy Requirement 6 regarding bundle safety characteristics, Task 2 and
Task 3 are created and addressed further in Sections 4.2 and 4.3.
Page | 49
Task 2
The modified bundle designs need to comply with the existing linear heat
rating, bundle power and channel power limits prescribed for standard
CANDU fuel. Specifically, the new designs must maintain a maximum
linear heat rating of less than 60 kW/m [44]. Ideally, the bundle must
have a ring power distribution that is similar to the existing bundles.
Task 3
Produce a radial temperature profile of the fuel pin with the highest
linear heat rating and compare it with the radial temperature profile of
the reference fuel pin of the same ring to ensure that adequate margins
to fuel centreline melting are maintained. The melting points of UO2
(2860 °C) and U-metal (1132 °C) are used as constraints here.
Page | 50
Requirement 1:
The enrichment of the enriched-fuel region is fixed at 19.5 wt% of U-235 which
is sufficiently high to allow Mo-99 extraction by existing processes while being slightly
below the 20 wt% limit for low-enriched fuel. According to an IAEA report [45], fuel
reprocessing technologies exist for both LEU metal and UO2 targets for Mo-99
production. Beside some modification needed to accommodate the larger masses of LEU
target material, the rest of the chemical processing involved for the production of Mo-99
using LEU targets is very similar to the present process for producing Mo-99 using HEU.
The expert committee report by the US National Academy of Sciences also
concluded that the there are no technical barriers to producing large quantities of Mo-99
from LEU targets [8].
For the modified fuel bundles proposed in this thesis, the Mo-99 producing fuel
pins are expected to be chemically processed using the modified acid dissolution
technique. After irradiation, the enriched fuel pellets are removed from the cladding and
processed for Mo-99 extraction. The mass and activity of Mo-99 that is expected to be
produced in these pins can be calculated from the output of the DRAGON code. The code
output is obtained for each specified lattice sub-region of the modified fuel bundle
geometrical model. The mass and activity of Mo-99 produced is also explored as part of
this thesis in Section 4.4. The expected yield of Mo-99 in six-day Curies is calculated for
each new bundle design.
Page | 51
3.3 Reactor Operating Conditions and Assumptions
The modified fuel bundles with different geometrical arrangements of 19.5 wt%
enriched, 0.2 wt% depleted and 0.71 wt% uranium fuels in different fuel rings are
subject to the same conditions and power limits as the existing fuel bundles in an
operating CANDU core. The new fuel bundle is designed to withstand irradiation in the
highest power channel of the 380-channel CANDU-6 reactor with a total thermal power
of approximately 2x109 Wth. A bundle power of 900 kW is used as the upper limit for a
typical CANDU fuel assembly in order to meet the existing channel power limits. The
maximum licensed bundle power limit for a CANDU-6 fuel-channel using 37-element fuel
bundle is 935 kW. This corresponds to a linear power rating in the hottest (outermost)
fuel element of approximately 60 kW/m.
Therefore, for all new designs considered, the lattice cell bundle power at
100% FP is assumed to correspond to the maximum instantaneous power of 900 kW.
The reference CANDU-6 fuel bundle contains 19.85 kg of uranium fuel. Hence, the
corresponding bundle specific power is 45.34 W/g (900 kW/19.85 kg per bundle). In
order to assess the safety margins of the proposed designs, the pin powers and linear
ratings are scaled according to the maximum operating CANDU-6 bundle specific power.
The bundle designs are analyzed using the reactor physics code DRAGON
version 3.05 ([32], [33], [34]). Transport calculations are performed using the collision
probability method as implemented in the DRAGON code. The model used for this study
is a single-cell infinite lattice with reflective boundaries on all sides. The effects of
reactivity devices are ignored in the single-cell DRAGON model.
Page | 52
The heat generated by the bundle is conducted through the fuel rod and
convected by the surrounding coolant in the fuel channel. In the current study, the fuel
temperature is calculated for the fuel pin with the highest linear heat rating at various
points along the radius of the pin, including the centre. The fuel temperature profile of
a 4th ring pin is calculated using a numerical integration method (see Section 3.4.2) for
each design and compared to the fuel melting limits.
The numerical integration method assumes a radial conduction model for a slice
of fuel element based on steady-state conditions where the fuel element geometry,
thermal properties, and physical characteristics are known. Axial conduction is assumed
negligible and thermal conductivity of the cladding material is assumed constant.
The melting points of UO2 (2860 °C) and U-metal (1132 °C) are used as the
maximum allowable fuel centreline temperatures. Steady-state cooling flow conditions
are assumed in the fuel channel resulting in a constant bulk coolant temperature.
Temperature of the coolant is assumed to be 276 °C, which is 10 °C higher than the
average CANDU-6 inlet temperature [46], added for conservatism in the analysis. The
difference in the proposed and reference CANDU temperature profiles and the available
margins to fuel melting limits provide high confidence in the adopted designs.
3.3.1 Reactor Fuelling Considerations
The use of modified fuel bundles for the production of Mo-99 will have an impact
on the regular refuelling cycles at CANDU stations. As previously explained, irradiation
times of about 15 to 20 days are sufficient to achieve maximum possible activity of
Page | 53
Mo-99. A burnup of 906.62 MWD/T, which corresponds to 20 days of irradiation at the
specific power of 45.33 kW/kg is used in this study.
The burnup time required to reach the maximum activity levels of Mo-99 is much
shorter than the normal time a regular fuel bundle spends inside the reactor (8 to 12
months depending on the location of the bundle in the core). As a consequence of the
shorter irradiation period, a fuelling machine visit is needed after the peak production
rate for Mo-99 is reached. To achieve steady production levels of Mo-99, two or more
modified fuel bundles can be loaded together at a time. By staggering the production in
multiple channels, a steady amount of Mo-99 producing bundles can be removed each
day to provide a constant yield.
Researchers from McMaster University have studied the impact of shorter
irradiation cycles for Mo-99 producing bundles on the standard fuelling operations [22].
This involved changing the total number of fuelling machine visits that may be required
in order to produce significant yields of Mo-99. The study simulated two different
fuelling scenarios consisting of 3 to 6 fuel channels containing 2 to 6 Mo-99 target
bundles in a staggered manner. The study concluded that with an additional 6 to 8
fuelling operations per week, a production level of 4 bundles per week is attainable [22].
Due to the unique flexibility of fuelling arrangement in CANDU reactors, a yield of
higher than 4 bundles per week is also possible. For the new designs proposed in this
study, the consequent changes in the existing fuelling schemes are not studied as no
difficulties are foreseen. The number of bundles to be extracted per week is assumed to
Page | 54
be a function of Mo-99 yield per bundle and the underlying commercial and medical
isotope market considerations.
Once an approximate activity of Mo-99 per bundle is known, a detailed
calculation based on the instantaneous channel parameters can be performed at various
stages in the fuelling cycle. The bundle fuelling scheme can then be optimized to
determine the most favourable irradiation times for each stage and bundle position for
the Mo-99 production bundles. Using multiple channels in a staggered manner would
ensure a yield of multiple bundles for a constant output of Mo-99 required for the target
medical isotopes market.
3.4 Design Options and Methodology
To develop a new 37-element fuel bundle aimed at producing large quantities of
Mo-99, five different design options are assessed. They include:
Page | 55
Design 1
19.5 wt% enriched UO2 fuel in the centre of the 4th ring fuel elements
encapsulated by 0.2 wt% depleted UO2 fuel. Fuel elements in the centre
and inner rings contain natural UO2.
Design 2
0.2 wt% depleted UO2 fuel in the centre of the 4th ring fuel elements
encapsulated by 19.5 wt% enriched UO2 fuel. Fuel elements in the centre
and inner rings contain natural UO2.
Design 3
0.2 wt% depleted U-metal fuel in the centre of the 4th ring fuel elements
encapsulated by 19.5 wt% enriched U-metal fuel. Fuel elements in the
centre and inner rings contain natural UO2.
Design 4
0.2 wt% depleted UO2 fuel in the centre of the fuel elements encapsulated
by 19.5 wt% enriched UO2 fuel in all four rings.
Design 5
0.2 wt% depleted U-metal fuel in the centre of the fuel elements
encapsulated by 19.5 wt% enriched U-metal fuel in all four rings.
Page | 56
A unit lattice cell is analyzed using the DRAGON neutron-transport code. The cell
is initially divided into 37 homogenous regions to represent different parts of the fuel
bundle including the four fuel rings, cladding, annulus gas, pressure tube and coolant.
Depending on the design, the regions are further split into sub-regions for accuracy and
higher resolution. For example, in Design 2 which contains an enriched uranium fuel
region encapsulated by depleted uranium fuel in the 4th ring and NU in other rings (see
Figure 3-1), the depleted and enriched fuel regions in the fuel pellet are further split into
10 and 3 sub-regions, respectively. In the remaining rings, a total of 4 sub-regions are
used to simulate the NU fuel pellet. Figure 3-2 illustrates the 46 (37 +9 additional
splitting) lattice sub-regions of the DRAGON geometrical model that is used to represent
the 37-element fuel bundle.
The multigroup transport equation is solved using the DRAGON code and the
69-group IAEA WIMS-D Library Update (WLUP) [34] for a single-cell lattice model to
find the neutron flux and cross-sections in each of these sub-regions integrated over all
energy groups. The fresh fuel kinf values are recorded for each case for assessment.
Data on lattice specifications for a 37-element CANDU fuel bundle is provided in
Appendix B.
Page | 57
Figure 3-2 37-Element CANDU Fuel Bundle and the Infinite Lattice Cell
Representation of Design 211
3.4.1 Method for Calculating the Linear Heat Rating
For the purpose of establishing the bounding linear heat rating for fuel pins of the
proposed bundles for Mo-99 production, this study assumes that a fresh target bundle
will be loaded in the middle of the highest power fuel channel facing a high thermal-
neutron flux and irradiated there for the duration of the irradiation period. In other
words, the position of the fuel bundle is assumed to be in position 6 or 7 out of a total of
12 fuel bundles in each CANDU fuel channel. This is a rather conservative case
considering the bundle would initially be loaded anywhere between position 1 to 12
11 The 37-element fuel bundle image is reproduced from the CANTEACH website [31]
Page | 58
depending on the fuelling scheme adopted, and hence could initially have a lower power
rating.
The maximum instantaneous bundle power located in the centre of the CANDU
core is 900 kWth. The pin power ratings are scaled according to the reference CANDU-6
bundle specific power as listed in Section 3.3. The procedure used to evaluate the linear
heat rating is provided within this section.
First, the density of uranium dv, U is computed, followed by the calculation of the
total linear density dL, U of the initial heavy elements in the fuel.
2
2v,
,v
UO
UUO
UA
Add (3.1)
regions
iiDUUL Vdd
1
2,v, (3.2)
where dv, UO2 is the density of natural uranium oxide fuel, AU is atomic mass of
natural uranium, AUO2 is atomic mass of uranium oxide, and V2-Di is the 2-D volume (cm2)
of each fuel region in the lattice cell.
The normalized linear heat rating QL’ for a fuel bundle is then given by
bundleULL PdQ ,
' (3.3)
where Pbundle is the normalized bundle specific power which is equal to 45.34 W/g
(based on 900 kW maximum bundle power), used for scaling with the reference
CANDU-6 bundle.
Page | 59
The unnormalized linear heat rating qi,u’ for each fuel region ‘i’ is given by:
'
, , 2ˆ
i u i f i i Dq e V (3.4)
where ei is the energy produced per fission, Σf,i is the macroscopic fission cross-
section at burnup, and ̂ is the condensed neutron energy group volume-integrated flux
at each region at burnup.
The total unnormalized linear heat rating QL,u’ for the entire fuel bundle is
therefore:
regions
i
uiuL qQ1
'
,
'
, (3.5)
The normalized linear heat power and the unnormalized linear heat rating for a
region within a fuel element are related by the following formula:
ui
uL
Li q
Q
QQ ,
'
'
,
'
'
(3.6)
In DRAGON, the multiple sub-regions (or splits) within one fuel type (enriched,
depleted, or natural) can be merged to provide cross-sections and fluxes for each fuel
type using volume averaging. The bundle length is also constant.
The linear power rating is important for fuel pins, but not for sub-regions inside
each fuel pin. Therefore, once the linear power in each fuel type within one fuel element
is known, the overall linear power for a fuel element composed of different fuel regions
(enriched + depleted) is the summation of two linear powers.
Page | 60
Finally, since there are rpinsN , pins associated with a ring, the average pin heat
rating, '
rQ , in ring ‘r’ can be computed by the following formula:
rpins
regionfueldepletedregionfuelenriched
rN
QQQ
,
''' (3.7)
3.4.2 Method for Calculating the Radial Temperature Profile
The heat generated in a fuel pin directly affects the fuel centreline temperature
and the temperature profile going from the fuel centre to the fuel surface. The fuel
centreline temperature and the temperature gradient are functions of thermal
conduction within the fuel pellet, heat transfer through the diametral fuel-sheath gap,
and conduction through the sheath, coolant temperature and sheath-to-coolant heat
transfer coefficient.
The primary heat transfer mechanisms within the diametral gap are conduction
through the fill gas and solid-to-solid contact conduction (fuel and sheath are in contact).
For the purpose of this work, the fuel pellet is assumed to remain in contact with the
cladding making the thickness of the gap between the fuel pellet and the cladding equal
to zero. This is a reasonable assumption considering that the Mo-99 producing fuel
bundles will use collapsible sheaths and are expected to be irradiated for a maximum of
20 days, which is not long enough for a gap to develop.
As part of the new fuel bundle development for Mo-99 production, a radial fuel
temperature profile of the 4th ring element of the proposed fuel bundles is produced and
compared against the fuel melting limits. The enriched fuel region in the fuel pellets adds
Page | 61
to the possibility of having higher centreline temperatures in the pin due to the increased
rate of fission and consequently higher power density in the region. Due to its proximity
to a large number of thermalized neutrons, the elements of the 4th ring present the most
conservative estimate for centreline calculations.
For the current study, the fuel centreline temperature is calculated using a
numerical integration method described below.
Numerical Integration Method
For any new fuel design, the interface between the fuel and the coolant is centrally
important to the design of the reactor because it limits the power output. The heat
transfer coefficient (hc) of the coolant is dependent on the fluid properties and flow
conditions. For liquid-to-wall heat transfer, the coefficient can be estimated by the use
of certain dimensionless fluid mechanic numbers:
Reynolds number
Prandtl number
Nusselt number
The Reynolds number is a measure of the relationship between the inertial and
viscous effects of the moving fluid and can be defined as [47]:
hVDRe
(3.8)
Page | 62
where ρ is density of the fluid, V is average fluid velocity, Dh is hydraulic radius of
the flow path, and μ is dynamic viscosity of the fluid.
wet
flow
hP
AD
4
(3.9)
where Aflow is the coolant flow area through the fuel bundle, and Pwet is the wetted
parameter.
The Prandtl number is a measure of the fluid thermal properties and can be
defined as:
k
c pPr
(3.10)
where cp is specific heat of the fluid, μ is dynamic viscosity of the fluid, and k is
thermal conductivity of the fluid. Some software such as NIST REFPROP can also provide
Prandtl number and other useful thermophysical properties of fluids at the specified
fluid state.
For the specific case of convective heat transfer inside a tube, the Nusselt number
is an empirical formula that is defined as:
4.08.0 PrRe023.0Nu (3.11)
where Re is Reynolds number, and Pr is Prandtl number. The relationship
between the Nusselt number and the heat transfer coefficient h can be defined as [48]:
Page | 63
k
hDNu h
(3.12)
For a solid, the general thermal energy balance equation of an arbitrary volume
can be expressed as:
dsntrQdVtrQdVt
e
ˆ),(''),('''
(3.13)
[stored] [generated] [transferred]
where ρ is the material density, e is the internal energy, V is the volume, S is the
surface area, Q''' is the volumetric heat generation, Q'' is the heat flux, and n̂ is the unit
vector on the surface. The internal energy can be replaced with temperature T times the
heat capacity c. Using Gauss law, the heat balance equation can be transformed into:
SV
dsnQQ ˆ'''' (3.14)
),(''),(''')(
trQtrQt
cT
(3.15)
Using Fourier law: ),(),('' trTktrQ , the equation governing the fuel
temperature distribution can be derived.
),(),(''')(
trTktrQt
cT
(3.16)
Page | 64
In order to calculate the fuel centreline temperature, steady-state one-
dimensional heat transfer with volumetric heat source and variation of thermal
conductivity with temperature is assumed.
),(),(''' trTktrQ f (3.17)
1( ( ) ) '''( )f
d dTk T r Q r
r dr dr (3.18)
( ( ) ) '''( )f
dTd k T r Q r rdr
dr (3.19)
Integrating both sides from the centreline to an arbitrary radius r:
0
( ) '''( )
r
f
dTk T r Q d
dr
(3.20)
Since
2
)(')('''
0
rQdQ
r
(3.21)
Therefore,
'( )( )
2f
dT Q rk T r
dr
(3.22)
'( )( )
2f
Q rk T dT dr
r
(3.23)
Page | 65
Integrating both sides again from an arbitrary radius r to the radius of the fuel
pin rf:
1 '( )( )
2
fsrT
f
T r
Qk T dT d
(3.24)
or, equivalently:
1 '( )( )
2
f
s
rT
f
T r
Qk T dT d
(3.25)
where,
35.16exp
6400
6142.3692.175408.7
100)(
2/52Tk f (3.26)
where = T/1000, T is in Kelvin, and kf is thermal conductivity for 95% dense
UO2 in W/m∙K. The above expression for thermal conductivity is taken from the IAEA
materials database [49]. The expression is plotted in Figure 3-3.
Figure 3-3: A Plot of UO2 Thermal Conductivity Showing Variation Due to
Temperature
2.0
2.5
3.0
3.5
4.0
4.5
5.0
5.5
400 600 800 1000 1200 1400 1600 1800
Th
erm
al
Co
nd
uct
ivit
y (
W/
m∙K
)
Temperature (K)
Page | 66
Since the temperature dependence of thermal conductivity kf(T) is known, the
left-hand side of Eq. (3.25) is a function, which can be calculated using the trapezoidal
rule to approximate the integral and equate with the right-hand side. Therefore, the
equation can be re-written as:
( , ) ( )
s
T
s f
T
F T T k T dT (3.27)
Or, equivalently:
1 '( )( , )
2
fr
s
r
QF T T d
(3.28)
The solution of Eq. (3.28) gives the temperature T as a function of radius r
corresponding to different points on the pin. If the radius r is taken to be zero
(integration from the centreline to the outer radius of the pin), then:
0
1 '( )( )
2
fcL
s
rT
f
T
Qk T dT d
(3.29)
Or, equivalently:
0
1 '( )( , )
2
fr
cL s
QF T T d
(3.30)
It is to be noted that the integrand in the right-hand side of Eq. (3.30) vanishes as
the radius approaches zero. In mathematical form:
Page | 67
0 L'Hopital's Rule 0 0
'( )
'( )lim lim lim 2 '''( ) 0
dQ
Q dQ
d
d
(3.31)
For a fuel pin that is divided into n annular regions of radii ri, the temperature at
boundaries between annuli will be denoted by T(ri)=Ti, where rn=rf and r0=0, and for
temperatures, T0=TcL and Tn=Ts. Each annulus will have the same index ‘i’ as its outer
radius.
In what follows, discrete forms of Eq. (3.21), Eq. (3.27) and Eq. (3.28) are
presented. The discrete forms of each equation are obtained by approximating the
integral in the respective equation. Because DRAGON, provides the average heat
generation rate for each annulus, Eq. (3.21) is approximated as:
2 2
1
1
'( )'''
2 2
ij j i
i
j
r r Q rQ
(3.32)
It can be observed that the above approximation provides the values of the linear
heat generation rate at the boundaries between annuli, which is at radii ri. To discretize
Eq. (3.27), kf(T) is assumed to be tabulated at discrete values Tk. using Eq. (3.26), and
with T0=Ts. Using the trapezoidal rule to approximate the integral, Eq. (3.27) becomes:
1
1
1
( ) ( )( , )
2
kf j f j
k s j j
j
k T k TF T T T T
(3.33)
For temperatures between the tabulation points Tk-1 and Tk, the function F can be
interpolated linearly as:
Page | 68
11 1
1
( , ) ( , )( , ) ( , ) k s k s
s k s k
k k
F T T F T TF T T F T T T T
T T
(3.34)
Because the values of the linear heat generation rate Q’ is calculated (according
to Eq. (3.32)) at radii ri, the integral in Eq. (3.28) can be approximated using the
trapezoidal rule:
11
1 1
'( ) '( )1( , )
2 2
nj jj j
i s
j i j j
r rQ r Q rF T T
r r
(3.35)
From a practical perspective, Eq. (3.35) is solved by finding the interval (Tk-1, Tk)
such that:
11
1
1 1
'( ) '( )1( , ) ( , )
2 2
nj jj j
k s k s
j i j j
r rQ r Q rF T T F T T
r r
(3.36)
And then solving:
111
1 1
11 1
'( ) '( )( , ) ( , ) 1( , )
2 2
nj jj jk s k s
k s i k
j ik k j j
r rQ r Q rF T T F T TF T T T T
T T r r
(3.37)
The fuel sheath (cladding) is exposed to constant heat flux. For the purpose of
this study, it is assumed that no gap exists between the fuel and cladding. Also since
Q’’’clad =0, heat conduction in the clad then becomes:
0)(1
dr
dTrk
dr
d
rc
(3.38)
Page | 69
)ln(2
'
)( 1
F
cF
n
i
i
scccladcr
trQ
TTkTk
(3.39)
Heat transfer from the clad to coolant can be represented by Newton’s law of
cooling (by convection).
)(''1
Bss
n
i
i TThQ
(3.40)
)(2
'
)(2
'''''
)( 1
2
11
cGs
n
i
i
cGs
i
n
i
i
s
n
i
i
BsCooltrh
Q
trh
rQ
h
Q
TTT
(3.41)
The phenomenon is dominated by the presence of a thin surface layer. The
temperature drop is assumed to occur over this thin layer and the bulk of the coolant is
assumed to have a constant temperature of 549 K.
3.4.3 Method for Calculating the Mass and Activity of Molybdenum-99
Produced
The IAEA-WLUP library [34] does not include fission yield data for Mo-99 and, as
a consequence, DRAGON cannot explicitly calculate the atomic density (or mass) of
Mo-99 produced from fission. Hence, the mass and activity of Mo-99 must be calculated
based on the total fission rates calculated by DRAGON. The following methodology is
used for calculating the mass and activity of Mo-99 produced.
Rate of change = Rate produced – Decay rate
Page | 70
NVcfdt
dNUenrichedfMo 235,99
ˆ (3.42)
where N is the number of Mo-99 atoms produced as a fission product, 99Mof is
the Mo-99 fission yield, f is the macroscopic fission cross-section at burnup (cm-1), c
is the DRAGON scaling multiplier, ̂ is the condensed neutron volume integrated flux in
the enriched region at burnup (n·cm/s), and 235, UenrichedV is the volume of the enriched
U-235 region in the bundle (cm3). Furthermore, the activation of Mo-99 by capturing a
neutron can be neglected here due to a small cross-section value of this reaction (σabs =
2.65 barns).
Let 235,99ˆ
UenrichedfMoprod VcfR (3.43)
The equation then becomes:
NRdt
dNprod (3.44)
NdtdtRdN prod (3.45)
dtRNdtdN prod (3.46)
Multiply both sides by eλt
dtReNdtedNe prod
ttt (3.47)
dteRNed t
prod
t )( (3.48)
Page | 71
Integrate both sides with-respect-to time
dteRNed
t
t
prod
t
t
00
)( (3.49)
The neutrons in the fuel region are not mono-energetic. There exists a spectrum
of neutron energy distribution. However, an energy condensed volume integrated
neutron flux is assumed here. As well, the corresponding average macroscopic cross-
sections are used. Hence the rate of production in this case is a constant, and Eq. (3.49)
then becomes:
dteRNed
t
t
prod
t
t
00
)( (3.50)
prodtprodtR
eR
NNe 0 (3.51)
Multiply both sides by e-λt
ttprodprodeNe
RRtN
0)( (3.52)
N0 is the initial number of Mo-99 items at t=0, which is equal to zero.
tprode
RtN
1)( (3.53)
Or, equivalently:
t
prod eRttN 1)()( (3.54)
Page | 72
t
UenrichedfMo eVcft
1ˆ)( 235,99 (Bq) (3.55)
where, )(t is activity at irradiation time t. The mass of Mo-99 produced then
becomes:
23
99
10023.6.1)(
x
Ae
Rtm Motprod
(3.56)
23
99235,99
10023.6.1
ˆ)(
x
Ae
Vcftm MotUenrichedfMo
(grams) (3.57)
where )(tm is the mass of Mo-99 produced due at irradiation time t, and 99MoA
is the atomic weight of Mo-99.
Eq. (3.56) and Eq. (3.57) above calculate the end-of-bombardment (EOB) activity
and mass of Mo-99 in fission products. The processing efficiency for Mo-99 is about 90%
and takes approximately one day, resulting in a post processing total that is equivalent
to 70.65% of the EOB value. The six-day Curies value is then computed as:
decayp
t
UenrichedfMo eVcft
1ˆ)( 235,99 (Bq) (3.58)
decayp
MotUenrichedfMo
x
Ae
Vcftm
23
99235,99
10023.6.1
ˆ)( (grams) (3.59)
Where p is the post processing efficient of 70.65%, and
decay is computed using:
22.0)6( )6(
0
days
decay eN
daysN (3.60)
Page | 73
Chapter 4
Assessment Results and Discussion
This chapter provides the results obtained from the DRAGON lattice code along
with the calculations of the linear heat ratings and fuel centreline temperatures for the
proposed designs.
As mentioned before, five different design options are assessed in this study.
Information on these proposed variations of the standard 37-element CANDU bundle
designs for Mo-99 production are provided in Sections 3.2 and 3.4. For each design, the
fuel pellets in the target rings are made up of two-regions, a region of enriched fuel
surrounded by a region of depleted uranium (or vice versa). Enrichment of 19.5 wt%
U-235, which is less than the threshold of HEU, was used in the modified designs. The
depleted uranium was assumed to have 0.20 wt% U-235 enrichment.
A single cell infinite lattice assembly was modelled using reactor physics code
DRAGON version 3.05. The DRAGON model considers a fresh fuel bundle at the start and
irradiates it for 20 days corresponding to a burnup of 906.62 MWD/T. This burn is
sufficient to reach the maximum activity of Mo-99 in the target fuel.
The Mo-99 production bundles are designed to meet the same safety and design
constraints as the standard 37-element CANDU fuel with respect to reactor neutronics
and heat generation in the fuel elements. The standard CANDU bundle with NU fuel is
used as a benchmark for new designs. The reference bundle assessment results are
provided in Tables 4-1 through 4-3 and Figures 4-1 and 4-2.
Page | 74
The DRAGON calculated fresh fuel kinf for the reference CANDU unitcell with NU
fuel bundle and heavy water coolant is found to be 1.1228. The kinf is greater than 1 since
the effects of adjuster rods and reactivity devices are not modelled in the DRAGON
unitcell lattice model. The reactivity devices absorb neutrons and result in the kinf being
closer to 1.
Table 4-1: Reference CANDU 37-Element Bundle Data Structures for Radial
Pin Power Profile Calculations
Region
Macroscopic Fission Cross-Section, Σf (cm-1)
Integrated Flux, ̂
(n·cm/s)
2-D Volume, V2-D
(cm2)
Unnormalized Linear Power Rating, qi.u (kW/cm)
Linear Density, dL, U (g/cm)
Normalized Linear Power
Rating , '
rQ
(kW/m) Ring 1 0.02236 0.3682 1.159 2.696E-16 10.83 37.68 Ring 2 0.02330 2.224 6.957 1.697E-15 65.00 39.53 Ring 3 0.02595 4.534 13.91 3.852E-15 130.0 44.87 Ring 4 0.03091 7.018 20.87 7.181E-15 195.0 55.76
Figure 4-1: Radial Pin Power Profile for Reference CANDU 37-Element Bundle
30
35
40
45
50
55
60
1 2 3 4LIN
EA
R H
EA
T R
AT
ING
(K
W/M
)
FUEL BUNDLE RINGS
Reference CANDU Fuel Bundle
Page | 75
Table 4-2: Reference CANDU 37-Element Bundle Normalized Heat Density and
Linear Power Rating in Ring 4 Sub-regions
Sub-regions in Ring 4
Enrichment (wt%)
Thickness (cm)
Pin Radii (cm)
Normalized Heat Density, Q’’’ (kW/cm3)
Cumulative Normalized Linear Power Rating, Q’ (kW/cm)
Ring4-Disk1 0.7110 0.03757 0.03757 468.5 2.077 Ring4-Disk2 0.7110 0.03757 0.07513 469.6 8.324 Ring4-Disk3 0.7110 0.03757 0.1127 469.7 18.73 Ring4-Disk4 0.7110 0.04948 0.1622 469.9 38.81 Ring4-Disk5 0.7110 0.04948 0.2117 470.9 66.18 Ring4-Disk6 0.7110 0.04938 0.2611 472.1 100.8 Ring4-Disk7 0.7110 0.04938 0.3106 473.5 142.9 Ring4-Disk8 0.7110 0.04948 0.3601 475.4 192.5 Ring4-Disk9 0.7110 0.04938 0.4096 477.6 249.6 Ring4-Disk10 0.7110 0.04938 0.4591 480.4 314.5 Ring4-Disk11 0.7110 0.04948 0.5085 483.7 387.3 Ring4-Disk12 0.7110 0.04938 0.5580 487.8 468.2 Ring4-Disk13 0.7110 0.04948 0.6075 493.5 557.6
Page | 76
Table 4-3: Reference CANDU 37-Element Bundle Numerical Integration
Results Using IAEA and Constant Thermal Conductivity for UO2
Node Temperature using IAEA Thermal Conductivity (°C)
Temperature using Constant Thermal Conductivity (°C)
Fuel Centreline 1919 2197 Node1 (Ring4) 1911 2190 Node2 (Ring4) 1887 2170 Node3 (Ring4) 1847 2135 Node4 (Ring4) 1770 2069 Node5 (Ring4) 1665 1978 Node6 (Ring4) 1533 1863 Node7 (Ring4) 1380 1724 Node8 (Ring4) 1211 1561 Node9 (Ring4) 1036 1373 Node10 (Ring4) 860.9 1161 Node11 (Ring4) 689.9 924.0 Node12 (Ring4) 526.6 661.4 Node13 (Ring4) 373.2 373.2 Node14 (Sheath) 309.7 309.7 Node15 (Coolant) 275.8 275.8
Page | 77
Figure 4-2: Reference CANDU 37-Element Bundle Radial Temperature Profile
of Ring 4 Pin Using IAEA and Constant Thermal Conductivity for UO2
0
500
1000
1500
2000
2500
3000
0.0 0.1 0.2 0.3 0.4 0.5 0.6 0.7 0.8
Te
mp
era
ture
(°C
)
Radial Distance (cm)
IAEA Thermal Conductivity (Eq.3.26)
Constant Thermal Conductivity(0.024 W/cm-K)
UO2 Melting Point
Page | 78
4.1 Task 1 - Comparison of Infinite Multiplicative Constants
Using an infinite lattice cell model, the fresh fuel kinf value of the new designs is
used to evaluate the viability of the design with respect to the reference CANDU kinf value.
The goal is to change the amount of 19.5 wt% U-235 enriched fuel used in the new
designs while maintaining the overall fuel bundle geometry such that the overall bundle
reactivity is compatible with the reference CANDU 37-element lattice.
For Designs 1, 2 and 3, the initial estimates of the thickness (or radius) of the
enriched fuel region are made based upon a simple mass balance relation with-respect-
to the mass of U-235 in new designs and the standard CANDU bundle, while ignoring
bundle physics related parameters such as bundle geometry, neutron flux and parasitic
absorptions. These estimations are provided in Appendix C.
The initial estimates are the starting point for inputting new fuel specifications in
the unitcell lattice simulations. The initial estimates are later adjusted based on their
deviation from the data collected using the reference CANDU lattice specifications.
Following the first few data points collection for new designs, the later data points are
synthesized through linear interpolation.
Designs 4 and 5 are slight variations of Designs 2 and 3, respectively, where the
initial concept of using mixed fuel (enriched + depleted) in Ring 4 elements are extended
to all rings for maximum yields of Mo-99 per bundle. Hence, the initial estimates for the
thickness of the enriched part was inferred from the parent designs (Design 2 or 3), and
altered accordingly based on the DRAGON simulation results.
Page | 79
Due to the higher fuel density of uranium metal compared to ceramic UO2 fuel,
Designs 3 and 5 present a challenge for balancing the mass of fuel in the pins, and
avoiding any resulting dissimilarity in bundle ring power distribution. The solution is to
find an optimal cladding thickness that would preserve the compatibility of bundle
reactivity with the existing CANDU bundle. The proposed thickness of the cladding
(2.27 mm) was calculated through mass balancing of both U-235 and U-238 in Design 3
and Design 5 fuel elements with the reference CANDU bundle.
The addition of enriched uranium in the Mo-99 target pins causes an increase in
fission rate resulting in a higher reactivity in that specific region. To compensate for this
increase reactivity, the remainder of the fuel pin is composed of depleted uranium.
Multiple cases with varying thickness (or radius) of the enriched region are
simulated in DRAGON for each design until a thickness (or radius) is determined with Δρ
value within the acceptable range (±1 mk). These cases are summarized in Tables 4-4
through 4-8 for each design. It is apparent from DRAGON results that the lattice
reactivity is very sensitive to changes in the amount of enriched region for the fixed
enrichment of 19.5 wt% U-235. Small changes in the amount of the enriched fuel
produce relatively large increase in reactivity.
Figures 4-3 through 4-7 illustrate the unitcell eigenvalue (k-infinity) as a function
of the thickness (or radius) of the enriched fuel region for the same overall fuel pin radius
as the reference bundle and compared with the kinf of the CANDU lattice.
Page | 80
Design 1
Table 4-4: Design 1 Unitcell Lattice k-infinity for Variations in Radius of
Enriched Central Region
Case # Radius of Enriched Central Target Region (mm)
Fresh Fuel k-infinity
∆ρ (mk)
1 1.00 1.0874 -29.0 2 1.10 1.1158 -5.64 3 1.20 1.1418 14.7 4* 1.14 1.1263 2.72 5* 1.127 1.1229 0.0301
* Value obtained through linear interpolation of data points
Figure 4-3: Design 1 Unitcell Lattice k-infinity Versus Variations in Radius of
Enriched Central Target Region (Fuel Pin Radius 6.075 mm)
1.060
1.070
1.080
1.090
1.100
1.110
1.120
1.130
1.140
1.150
1 mm 1.1 mm 1.2 mm 1.14 mm 1.127 mm
K-I
NF
INIT
Y
Design 1 Reference CANDU
Page | 81
Design 2
Table 4-5: Design 2 Unitcell Lattice k-infinity for Variation in Thickness of
Enriched Annular Region
Case #
Thickness of Enriched Annular Target Region (mm)
Fresh Fuel k-infinity
∆ρ (mk)
1 0.0750 1.1067 -13.0 2 0.125 1.1961 54.5 3 0.0850 1.1267 3.07 4* 0.0830 1.1228 0.00793
* Value obtained through linear interpolation of data points
Figure 4-4: Design 2 Unitcell Lattice k-infinity Versus Variations in Thickness
of Enriched Annular Target Region (Fuel Pin Radius 6.075 mm)
1.070
1.090
1.110
1.130
1.150
1.170
1.190
0.075 mm 0.125 mm 0.085 mm 0.083 mm
K-I
NF
INIT
Y
Design 2 Reference CANDU
Page | 82
Design 3
Table 4-6: Design 3 Unitcell Lattice k-infinity for Variation in Thickness of
Enriched Annular Region
Case #
Thickness of Enriched Annular Target Region (mm)
Fresh Fuel k-infinity
∆ρ (mk)
1 0.0660 1.1357 10.1 2 0.0560 1.1090 -11.1 3* 0.0610 1.1227 -0.108
* Value obtained through linear interpolation of data points
Figure 4-5: Design 3 Unitcell Lattice k-infinity Versus Variations in Thickness
of Enriched Annular Target Region (Fuel Pin Radius 4.266 mm)
1.070
1.080
1.090
1.100
1.110
1.120
1.130
1.140
1.150
1.160
0.066 mm 0.056 mm 0.061 mm
K-I
NF
INIT
Y
Design 3 Reference CANDU
Page | 83
Design 4
Table 4-7: Design 4 Unitcell Lattice k-infinity for Variation in Thickness of
Enriched Annular Region
Case #
Thickness of Enriched Annular Target Region (mm)
Fresh Fuel k-infinity
∆ρ (mk)
1 0.0830 1.1248 1.54 2 0.0820 1.1212 -1.29 3* 0.0825 1.1230 0.128
* Value obtained through linear interpolation of data points
Figure 4-6: Design 4 Unitcell Lattice k-infinity Versus Variations in Thickness
of Enriched Annular Target Region (Fuel Pin Radius 6.075 mm)
1.080
1.090
1.100
1.110
1.120
1.130
1.140
1.150
0.0830 mm 0.0820 mm 0.0825 mm
K-I
NF
INIT
Y
Design 4 Reference CANDU
Page | 84
Design 5
Table 4-8: Design 5 Unitcell Lattice k-infinity for Variation in Thickness of
Enriched Annular Region
Case #
Thickness of Enriched Annular Region (mm)
Fresh Fuel k-infinity
∆ρ (mk)
1 0.0610 1.1201 -2.15 2 0.0620 1.1246 1.37 3* 0.0616 1.1228 -0.0325
* Value obtained through linear interpolation of data points
Figure 4-7: Design 5 Unitcell Lattice k-infinity Versus Variations in
Thickness of Enriched Annular Target Region (Fuel Pin Radius 4.266 mm)
1.080
1.090
1.100
1.110
1.120
1.130
1.140
1.150
0.061 mm 0.062 mm 0.0616 mm
K-I
NF
INIT
Y
Design 5 Reference CANDU
Page | 85
4.2 Task 2 - Comparison of Linear Heat Rating
The new designs must maintain a maximum power rating licensing limit of
60 kW/m to allow for existing operational practices to be maintained. Furthermore, to
avoid dissimilar power peaking effects in the bundle, the new designs are intended to
mimic the existing 37-element bundle radial pin power profile.
As mentioned in the previous section, in order to deal with the increased
reactivity of the fuel pins containing enriched fuel region over NU fuel, the remaining fuel
material in the pins is made up of depleted uranium. Once the thickness (or radius) of
the enriched region in the pins for each design is selected in Task 1 whereby the total
change in reactivity is within ±1mk with-respect-to the reference CANDU lattice, the
designs with those particular thicknesses (or radii) are further investigated for
evaluation and calculation of the element linear heat rating and fuel centreline
temperatures.
Data structures for macroscopic fission cross-sections, condensed neutron
volume integrated flux, and 2-D volume etc., for each fuel region are obtained from
DRAGON and processed for calculating the bundle radial pin power profile. The linear
heat rating is calculated using the methodology described in Section 3.4.1. The DRAGON
data structures for linear heat rating calculations are provided in Tables 4-9 through
4-13.
Figures 4-8 through 4-12 show the power profiles of the new designs versus the
reference CANDU bundle located in the highest power channel in the core. The
Page | 86
corresponding bundle specific power is 45.34 W/g (based on 900 kW bundle power). All
the pin powers and linear ratings are scaled to this specific power.
As expected, the power profile is lowest in the centre and higher in the outer rings
due to the corresponding neutron flux at these locations. The radial pin power profiles
of Mo-99 target bundles are also very similar to the reference CANDU radial pin profile,
whereby all designs meets the linear heat rating licensing limit of 60 kW/m with
adequate margins.
The linear heat rating of the target elements in the modified fuel bundle designs
was a priori postulated to be higher than the reference CANDU bundle due to the
presence of enriched fuel region. The resemblances of the two curves is not quite
unexpected. Efforts to keep the fresh fuel kinf value for a partially enriched fuel bundles
as close as possible to the reference CANDU lattice resulted in a configuration which
consisted of a relatively large depleted uranium region and a relatively small enriched
fuel region in these pins. The volumetric ratio of enriched fuel to depleted fuel was
3.56% in Design 1, 2.79% in Design 2 and 4, and 2.92% in Design 3 and 5. Therefore, the
increase in the fission rate and thus power density in the enriched region is compensated
by the relative decrease of power density in the depleted region, resulting in an overall
linear heat rating profile similar to the reference CANDU fuel bundle.
Page | 87
Design 1
Table 4-9: Design 1 Data for Radial Pin Power Profile Calculations
Region
Macroscopic Fission Cross-Section, Σf (cm-1)
Integrated Flux, ̂
(n·cm/s)
2-D Volume, V2-D (cm2)
Unnormalized Linear Power Rating, qi.u (kW/cm)
Linear Density, dL, U (g/cm)
Normalized Linear Power
Rating , '
rQ
(kW/m) Ring 1 0.02232 0.3637 1.159 2.658E-16 10.83 37.14 Ring 2 0.02331 2.194 6.956 1.675E-15 65.00 39.01 Ring 3 0.02593 4.484 13.91 3.807E-15 130.0 44.33 Ring 4 (Enriched)
0.5216 0.2538 0.7182 4.299E-15 6.711 56.32
Ring 4 (Depleted)
0.01329 6.714 20.15 2.957E-15 188.2
Figure 4-8: Design 1 Bundle Radial Pin Power Profile
30
35
40
45
50
55
60
1 2 3 4
LIN
EA
R H
EA
T R
AT
ING
(K
W/M
)
FUEL BUNDLE RINGS
Design 1 Reference CANDU
Page | 88
Design 2
Table 4-10: Design 2 Data for Radial Pin Power Profile Calculations
Region
Macroscopic Fission Cross-Section, Σf (cm-1)
Integrated Flux, ̂
(n·cm/s)
2-D Volume, V2-D
(cm2)
Unnormalized Linear Power Rating, qi.u (kW/cm)
Linear Density, dL, U (g/cm)
Normalized Linear Power
Rating , '
rQ
(kW/m) Ring 1 0.02236 0.3658 1.159 2.678E-16 10.83 37.43 Ring 2 0.02327 2.211 6.956 1.685E-15 65.00 39.26 Ring 3 0.02586 4.513 13.91 3.821E-15 130.0 44.50 Ring 4 (Depleted)
0.01337 6.771 20.30 2.999E-15 189.7 56.11
Ring 4 (Enriched)
0.6737 0.1932 0.5664 4.227E-15 5.292
Figure 4-9: Design 2 Bundle Radial Pin Power Profile
30
35
40
45
50
55
60
1 2 3 4
LIN
EA
R H
EA
T R
AT
ING
(K
W/M
)
FUEL BUNDLE RINGS
Design 2 Reference CANDU
Page | 89
Design 3
Table 4-11: Design 3 Data for Radial Pin Power Profile Calculations
Region
Macroscopic Fission Cross-Section, Σf (cm-1)
Integrated Flux, ̂
(n·cm/s)
2-D Volume, V2-D
(cm2)
Unnormalized Linear Power Rating, qi.u (kW/cm)
Linear Density, dL, U (g/cm)
Normalized Linear Power
Rating , '
rQ
(kW/m) Ring 1 0.02243 0.3673 1.159 2.698E-16 10.83 37.67 Ring 2 0.02335 2.224 6.956 1.700E-15 65.00 39.58 Ring 3 0.02616 4.530 13.91 3.880E-15 130.0 45.15 Ring 4 (Depleted)
0.02589 3.336 9.999 2.860E-15 189.4 55.56
Ring 4 (Enriched)
1.319 0.1004 0.2922 4.302E-15 5.537
Figure 4-10: Design 3 Bundle Radial Pin Power Profile
30
35
40
45
50
55
60
1 2 3 4
LIN
EA
R H
EA
T R
AT
ING
(K
W/M
)
FUEL BUNDLE RINGS
Design 3 Reference CANDU
Page | 90
Design 4
Table 4-12: Design 4 Data for Radial Pin Power Profile Calculations
Region
Macroscopic Fission Cross-Section, Σf (cm-1)
Integrated Flux, ̂
(n·cm/s)
2-D Volume, V2-D
(cm2)
Unnormalized Linear Power Rating, qi.u (kW/cm)
Linear Density, dL, U (g/cm)
Normalized Linear Power
Rating , '
rQ
(kW/m) Ring 1 (Depleted)
0.009508 0.3546 1.128 55.87 10.54 37.70
Ring 1 (Enriched)
0.4927 0.009897 0.03128 1.549 0.2922
Ring 2 (Depleted)
0.009894 2.143 6.769 335.2 63.24 39.52
Ring 2 (Enriched)
0.5111 0.05991 0.1877 9.294 1.753
Ring 3 (Depleted)
0.01100 4.372 13.53 670.5 126.5 44.90
Ring 3 (Enriched)
0.5686 0.1225 0.3753 18.59 3.507
Ring 4 (Depleted)
0.013348 6.760 20.30 1005 189.7 55.74
Ring 4 (Enriched)
0.6729 0.1918 0.5630 27.88 5.260
Figure 4-11: Design 4 Bundle Radial Pin Power Profile
30
35
40
45
50
55
60
1 2 3 4
LIN
EA
R H
EA
T R
AT
ING
(K
W/M
)
FUEL BUNDLE RINGS
Design 4 Reference CANDU
Page | 91
Design 5
Table 4-13: Design 5 Data for Radial Pin Power Profile Calculations
Region
Macroscopic Fission Cross-Section, Σf (cm-1)
Integrated Flux, ̂
(n·cm/s)
2-D Volume, V2-D
(cm2)
Unnormalized Linear Power Rating, qi.u (kW/cm)
Linear Density, dL, U (g/cm)
Normalized Linear Power
Rating , '
rQ
(kW/m) Ring 1 (Depleted)
0.01873 0.1755 0.5553 1.089E-16 10.52 38.52
Ring 1 (Enriched)
0.9797 0.005259 0.01639 1.673E-16 0.3106
Ring 2 (Depleted)
0.01945 1.057 3.332 6.811E-16 63.14 39.89
Ring 2 (Enriched)
0.9896 0.03221 0.09835 1.035E-15 1.863
Ring 3 (Depleted)
0.02155 2.1509 6.664 1.535E-15 126.2 45.17
Ring 3 (Enriched)
1.110 0.06521 0.1967 2.350E-15 3.727
Ring 4 (Depleted)
0.02581 3.315 9.996 2.833E-15 189.4 55.40
Ring 4 (Enriched)
1.316 0.1009 0.2951 4.315E-15 5.591
Figure 4-12: Design 5 Bundle Radial Pin Power Profile
30
35
40
45
50
55
60
1 2 3 4
LIN
EA
R H
EA
T R
AT
ING
(K
W/M
)
FUEL BUNDLE RINGS
Design 5 Reference CANDU
Page | 92
4.3 Task 3 - Comparison of Radial Temperature Profiles
Another important fuel design parameter is fuel centreline temperature. The
margins available for fuel melting under normal operations and various accidental
scenarios play an important role in fuel bundle design and design optimization. In
addition to fuel centreline temperature, the sheath temperature must also be kept below
the accepted limits established by the industry.
The melting point of UO2 and U-metal is 2865 °C and 1132 °C, respectively. For
the purpose of this work, it is assumed that no gap is developed between the fuel and
cladding due to the short irradiation period required to reach peak activities of Mo-99.
The variation in UO2 thermal conductivity as a function of fuel temperature is accounted
for by utilizing the IAEA UO2 thermal conductivity relation (Eq. 3.26). A second radial
temperature profile is produced using a conservative value of UO2 thermal conductivity
(0.024 W/cm∙k). The thermal conductivity of U-metal is 0.43 W/cm∙k.
The fuel temperature calculations are greatly dependent on the heat conduction
coefficient used. The intent of the analysis is to compare the radial temperature profiles
of the highest power element of the new designs to the reference CANDU bundle profile,
and to ensure that the fuel centreline melting criterion is satisfied. This is illustrated in
Figures 4-13 through 4-20.
Thermophysical properties of coolant obtained using NIST REFPROP are
provided in Table 4-14. Table 4-15 lists the CANDU specific important heat transfer
parameters required for radial temperature profile calculations.
Page | 93
Additional data on materials and lattice specifications for 37-element CANDU fuel
bundle are provided in Appendix B. A numerical integration methodology as described
in Section 3.4.2 is used to calculate the radial temperature profiles for all designs, and
summarized in Tables 4-16 through 4-25.
Using the numerical integration method, the centreline temperatures of the
Mo-99 target bundles are calculated and found to satisfy the centreline melting criterion
for all new designs with the exception of Design 1 (See Figures 4-13 and 4-14). This is
not unexpected. The UO2 centreline temperature has always been a concern for the
industry due to relatively low thermal conductivity of ceramic UO2. In the case of
Design 1, the 19.5 wt% U-235 enriched fuel region is located in the centre of the Mo-99
target pins. The enriched fuel region with its high power density is encapsulated by a
relatively large volume of depleted fuel with much lower power density (see Table 4-16).
The power density of the enriched region is approximately 43 times higher than the
depleted region. Hence, the majority of the power production takes place towards the
centre of the pin resulting in significantly high centreline temperatures.
For the remaining designs, the fuel centreline temperature is lower than the
reference fuel. This is due to the relatively small thickness of the enriched fuel region on
the periphery of the fuel elements.
For the same steady-state channel conditions used in this analysis, the ΔT across
the thicker cladding used in Designs 3 and 5 is much higher compared to the reference
bundle. This is compensated by the much higher thermal conductivity of the U-metal
Page | 94
(0.43 W/cm∙K) as compared to ceramic UO2. The resulting centreline temperatures
provide adequate margins to centreline melting.
Table 4-14: Thermophysical Properties of Coolant Using NIST REFPROP [46]
Temperature (°C)
Pressure (MPa)
Density (kg/m3)
Viscosity (Pa∙s) x 10-6
Prandtl Number
Channel Inlet
266 11.05 781.9 101.0 0.8215
Channel Outlet
312 10.29 686.5 81.41 0.9534
Table 4-15: CANDU Specific Important Heat Transfer Parameters [46]
Parameter Value
Average Coolant Velocity through the Channel, V 10 m/s Coolant Flow Area, A 0.003507 m2
Wetted Perimeter, Pw 1.847 m Hydraulic Diameter, Dh 0.007595 m Reynolds Number, Re 305661 Nusselt Number, Nu 536.0 Coolant Heat Transfer Coefficient, HC 4.006 W/cm2∙K Thermal Conductivity of Clad, kC 0.107 W/cm∙K Thermal Conductivity of UO2 0.024 W/cm∙K Thermal Conductivity of U-Metal 0.430 W/cm∙K
Page | 95
Design 1
Table 4-16: Design 1 Normalized Heat Density and Linear Power Rating in
Ring 4 Sub-regions
Sub-regions in Ring 4
Enrichment (wt %)
Thickness (cm)
Pin Radii (cm)
Normalized Heat Density, Q’’’ (kW/cm3)
Cumulative Normalized Linear Power Rating, Q’ (kW/cm)
Enriched1 19.50 0.03757 0.03757 7797 34.57 Enriched2 19.50 0.03757 0.07513 8057 141.7 Enriched3 19.50 0.03757 0.1127 8659 333.7 Depleted1 0.2000 0.04948 0.1622 194.8 342.0 Depleted2 0.2000 0.04948 0.2117 198.5 353.5 Depleted3 0.2000 0.04948 0.2611 200.6 368.3 Depleted4 0.2000 0.04948 0.3106 202.0 386.2 Depleted5 0.2000 0.04948 0.3601 203.3 407.4 Depleted6 0.2000 0.04948 0.4096 204.4 431.9 Depleted7 0.2000 0.04948 0.4591 205.5 459.7 Depleted8 0.2000 0.04948 0.5085 206.7 490.8 Depleted9 0.2000 0.04948 0.5580 207.9 525.2 Depleted10 0.2000 0.04948 0.6075 209.5 563.2
Page | 96
Table 4-17: Design 1 Numerical Integration Results Using IAEA and Constant
Thermal Conductivity for UO2
Node Temperature Using IAEA Thermal Conductivity (°C)
Temperature Using Constant Thermal Conductivity (°C)
Fuel Centreline 4486 5862 Node1 (Enriched1) 4428 5748 Node2 (Enriched2) 4247 5398 Node3 (Enriched3) 3921 4794 Node4 (Depleted1) 3425 3962 Node5 (Depleted2) 2996 3342 Node6 (Depleted3) 2580 2837 Node7 (Depleted4) 2149 2401 Node8 (Depleted5) 1705 2012 Node9 (Depleted6) 1305 1653 Node10 (Depleted7) 987.3 1316 Node11 (Depleted8) 738.1 993.5 Node12 (Depleted9) 538.4 680.7 Node13 (Depleted10) 374.1 374.1 Node14 (Sheath) 310.0 310.0 Node15 (Coolant) 275.8 275.8
Page | 97
Figure 4-13: Design 1 Radial Temperature Profile of Ring 4 Pin Using IAEA
Thermal Conductivity for UO2
0
500
1000
1500
2000
2500
3000
3500
4000
4500
5000
0.0 0.1 0.2 0.3 0.4 0.5 0.6 0.7 0.8
Te
mp
era
ture
(°C
)
Radial Distance (cm)
Design 1
ReferenceCANDU
EnrichedRegion
DepletedRegion
Fuel Centreline
UO2 Melting Point
Page | 98
Figure 4-14: Design 1 Radial Temperature Profile of Ring 4 Pin Using a
Constant Thermal Conductivity for UO2 (0.024 W/cm∙K)
0
1000
2000
3000
4000
5000
6000
7000
0.0 0.1 0.2 0.3 0.4 0.5 0.6 0.7 0.8
Te
mp
era
ture
(°C
)
Radial Distance (cm)
Design 1
ReferenceCANDU
EnrichedRegion
DepletedRegion
Fuel Centreline
UO2 Melting Point
Page | 99
Design 2
Table 4-18: Design 2 Normalized Heat Density and Linear Power Rating in
Ring 4 Sub-regions
Sub-regions in Ring 4
Enrichment (wt %)
Thickness (cm)
Pin Radii (cm)
Normalized Heat Density, Q’’’ (kW/cm3)
Cumulative Normalized Linear Power Rating, Q’ (kW/cm)
Depleted1 0.2000 0.05992 0.05992 204.5 2.306 Depleted2 0.2000 0.05992 0.1198 204.6 9.233 Depleted3 0.2000 0.05992 0.1798 204.7 20.78 Depleted4 0.2000 0.05992 0.2397 205.1 36.97 Depleted5 0.2000 0.05992 0.2996 205.3 57.82 Depleted6 0.2000 0.05992 0.3595 205.7 83.35 Depleted7 0.2000 0.05992 0.4194 206.2 113.6 Depleted8 0.2000 0.05992 0.4794 206.7 148.5 Depleted9 0.2000 0.05992 0.5393 207.3 188.3 Depleted10 0.2000 0.05992 0.5992 207.8 232.8 Enriched1 19.50 0.002767 0.6020 10444 341.9 Enriched2 19.50 0.002767 0.6047 10384 450.8 Enriched3 19.50 0.002767 0.6075 10466 561.1
Page | 100
Table 4-19: Design 2 Numerical Integration Results Using IAEA and Constant
Thermal Conductivity for UO2
Node Temperature Using IAEA Thermal Conductivity (°C)
Temperature Using Constant Thermal Conductivity (°C)
Fuel Centreline 874.8 1178 Node1 (Depleted1) 868.8 1171 Node2 (Depleted2) 851.1 1148 Node3 (Depleted3) 822.0 1109 Node4 (Depleted4) 782.5 1056 Node5 (Depleted5) 733.4 987.1 Node6 (Depleted6) 676.1 902.7 Node7 (Depleted7) 611.9 802.9 Node8 (Depleted8) 542.1 687.5 Node9 (Depleted9) 468.3 556.5 Node10 (Depleted10) 391.7 409.9 Node11 (Enriched1) 387.3 401.1 Node12 (Enriched2) 381.3 389.1 Node13 (Enriched3) 373.8 373.8 Node14 (Sheath) 309.9 309.9 Node15 (Coolant) 275.8 275.8
Page | 101
Figure 4-15: Design 2 Radial Temperature Profile of Ring 4 Pin Using IAEA
Thermal Conductivity for UO2
0
500
1000
1500
2000
2500
3000
0.0 0.1 0.2 0.3 0.4 0.5 0.6 0.7 0.8
Te
mp
era
ture
(°C
)
Radial Distance (cm)
Design 2
ReferenceCANDU
EnrichedRegion
DepletedRegion
Fuel Centreline
UO2 Melting Point
320
370
420
470
0.590 0.600 0.610 0.620
Tem
per
atu
re (
°C)
Radial Distance (cm)
Page | 102
Figure 4-16: Design 2 Radial Temperature Profile of Ring 4 Pin Using a
Constant Thermal Conductivity for UO2 (0.024 W/cm∙K)
0
500
1000
1500
2000
2500
3000
0.0 0.1 0.2 0.3 0.4 0.5 0.6 0.7 0.8
Te
mp
era
ture
(°C
)
Radial Distance (cm)
Design 2
ReferenceCANDU
EnrichedRegion
DepletedRegion
Fuel Centreline
UO2 Melting Point
320
370
420
470
0.59 0.60 0.61 0.62
Te
mp
era
ture
(°C
)
Radial Distance (cm)
Page | 103
Design 3
Table 4-20: Design 3 Normalized Heat Density and Linear Power Rating in
Ring 4 Sub-regions
Sub-regions in Ring 4
Enrichment (wt %)
Thickness (cm)
Pin Radii (cm)
Normalized Heat Density, Q’’’ (kW/cm3)
Cumulative Normalized Linear Power Rating, Q’ (kW/cm)
Depleted1 0.2000 0.04205 0.04205 394.6 2.192 Depleted2 0.2000 0.04205 0.08410 394.8 8.772 Depleted3 0.2000 0.04205 0.1261 395.3 19.75 Depleted4 0.2000 0.04205 0.1682 396.0 35.15 Depleted5 0.2000 0.04205 0.2102 396.8 54.99 Depleted6 0.2000 0.04205 0.2523 397.6 79.28 Depleted7 0.2000 0.04205 0.2943 398.6 108.0 Depleted8 0.2000 0.04205 0.3364 400.2 141.4 Depleted9 0.2000 0.04205 0.3784 401.8 179.3 Depleted10 0.2000 0.04205 0.4205 403.0 221.9 Enriched1 19.50 0.002033 0.4225 20392 331.7 Enriched2 19.50 0.002033 0.4246 20478 442.5 Enriched3 19.50 0.002033 0.4266 20800 555.6
Page | 104
Table 4-21: Design 3 Numerical Integration Results Using Constant Thermal
Conductivity for U-Metal
Node Temperature Using Constant Thermal Conductivity (°C)
Fuel Centreline 793.0 Node1 (Depleted1) 792.6 Node2 (Depleted2) 791.4 Node3 (Depleted3) 789.3 Node4 (Depleted4) 786.5 Node5 (Depleted5) 782.8 Node6 (Depleted6) 778.4 Node7 (Depleted7) 773.1 Node8 (Depleted8) 766.9 Node9 (Depleted9) 760.0 Node10 (Depleted10) 752.2 Node11 (Enriched1) 751.7 Node12 (Enriched2) 751.0 Node13 (Enriched3) 750.1 Node14 (Sheath) 309.6 Node15 (Coolant) 275.8
Page | 105
Figure 4-17: Design 3 Radial Temperature Profile of Ring 4 Pin Using a
Constant Thermal Conductivity for U-Metal (0.43 W/cm∙K)
0
500
1000
1500
2000
2500
3000
0.0 0.1 0.2 0.3 0.4 0.5 0.6 0.7 0.8
Te
mp
era
ture
(°C
)
Radial Distance (cm)
Design 3
ReferenceCANDU
EnrichedRegion
DepletedRegion
Fuel Centreline
UO2 Melting Point
U-Metal Melting Point
720
740
760
780
0.41 0.42 0.43 0.44
Tem
per
atu
re (
°C)
Radial Distance (cm)
Page | 106
Design 4
Table 4-22: Design 4 Normalized Heat Density and Linear Power Rating in
Ring 4 Sub-regions
Sub-regions in Ring 4
Enrichment (wt %)
Thickness (cm)
Pin Radii (cm)
Normalized Heat Density, Q’’’ (kW/cm3)
Cumulative Normalized Linear Power Rating, Q’ (kW/cm)
Depleted1 0.2000 0.05993 0.05993 203.7 2.298 Depleted2 0.2000 0.05993 0.1198 203.8 9.199 Depleted3 0.2000 0.05993 0.1798 203.9 20.70 Depleted4 0.2000 0.05993 0.2397 204.3 36.84 Depleted5 0.2000 0.05993 0.2996 204.6 57.61 Depleted6 0.2000 0.05993 0.3595 205.0 83.05 Depleted7 0.2000 0.05993 0.4195 205.4 113.2 Depleted8 0.2000 0.05993 0.4794 206.0 148.0 Depleted9 0.2000 0.05993 0.5393 206.6 187.7 Depleted10 0.2000 0.05993 0.5993 207.1 232.1 Enriched1 19.50 0.002750 0.6020 10410 340.1 Enriched2 19.50 0.002750 0.6048 10358 448.1 Enriched3 19.50 0.002750 0.6075 10435 557.4
Page | 107
Table 4-23: Design 4 Numerical Integration Results Using IAEA and Constant
Thermal Conductivity for UO2
Node Temperature Using IAEA Thermal Conductivity (°C)
Temperature Using Constant Thermal Conductivity (°C)
Fuel Centreline 871.3 1175 Node1 (Depleted1) 865.4 1167 Node2 (Depleted2) 847.7 1144 Node3 (Depleted3) 818.9 1106 Node4 (Depleted4) 779.6 1052 Node5 (Depleted5) 730.8 984.1 Node6 (Depleted6) 673.8 900.0 Node7 (Depleted7) 609.9 800.4 Node8 (Depleted8) 540.6 685.5 Node9 (Depleted9) 467.1 554.9 Node10 (Depleted10) 390.9 408.8 Node11 (Enriched1) 386.5 400.2 Node12 (Enriched2) 380.6 388.2 Node13 (Enriched3) 373.1 373.1 Node14 (Sheath) 309.7 309.7 Node15 (Coolant) 275.8 275.8
Page | 108
Figure 4-18: Design 4 Radial Temperature Profile of Ring 4 Pin Using IAEA
Thermal Conductivity for UO2
0
500
1000
1500
2000
2500
3000
0.0 0.1 0.2 0.3 0.4 0.5 0.6 0.7 0.8
Te
mp
era
ture
(°C
)
Radial Distance (cm)
Design 4
ReferenceCANDU
EnrichedRegion
DepletedRegion
Fuel Centreline
Page | 109
Figure 4-19: Design 4 Radial Temperature Profile of Ring 4 Pin Using a
Constant Thermal Conductivity for UO2 (0.024 W/cm∙K)
0
500
1000
1500
2000
2500
3000
0.0 0.1 0.2 0.3 0.4 0.5 0.6 0.7 0.8
Te
mp
era
ture
(°C
)
Radial Distance (cm)
Design 4
ReferenceCANDU
EnrichedRegion
DepletedRegion
Fuel Centreline
UO2 Melting Point
Page | 110
Design 5
Table 4-24: Design 5 Normalized Heat Density and Linear Power Rating in
Ring 4 Sub-regions
Sub-regions in Ring 4
Enrichment (wt %)
Thickness (cm)
Pin Radii (cm)
Normalized Heat Density, Q’’’ (kW/cm3)
Cumulative Normalized Linear Power Rating, Q’ (kW/cm)
Depleted1 0.2000 0.04204 0.04204 390.5 2.169 Depleted2 0.2000 0.04204 0.08409 390.6 8.678 Depleted3 0.2000 0.04204 0.1261 391.2 19.54 Depleted4 0.2000 0.04204 0.1682 391.8 34.77 Depleted5 0.2000 0.04204 0.2102 392.7 54.40 Depleted6 0.2000 0.04204 0.2523 393.4 78.44 Depleted7 0.2000 0.04204 0.2943 394.5 106.9 Depleted8 0.2000 0.04204 0.3364 396.0 139.9 Depleted9 0.2000 0.04204 0.3784 397.7 177.4 Depleted10 0.2000 0.04204 0.4204 398.9 219.5 Enriched1 19.50 0.002053 0.4225 20223 329.5 Enriched2 19.50 0.002053 0.4245 20329 440.6 Enriched3 19.50 0.002053 0.4266 20653 554.0
Page | 111
Table 4-25: Design 5 Numerical Integration Results Using Constant Thermal
Conductivity for U-Metal
Node Temperature Using Constant Thermal Conductivity (°C)
Fuel Centreline 791.2 Node1 (Depleted1) 790.8 Node2 (Depleted2) 789.6 Node3 (Depleted3) 787.6 Node4 (Depleted4) 784.8 Node5 (Depleted5) 781.1 Node6 (Depleted6) 776.7 Node7 (Depleted7) 771.5 Node8 (Depleted8) 765.4 Node9 (Depleted9) 758.5 Node10 (Depleted10) 750.8 Node11 (Enriched1) 750.3 Node12 (Enriched2) 749.6 Node13 (Enriched3) 748.7 Node14 (Sheath) 309.5 Node15 (Coolant) 275.8
Page | 112
Figure 4-20: Design 5 Radial Temperature Profile of Ring 4 Pin Using a
Constant Thermal Conductivity for U-Metal (0.43 W/cm∙K)
0
500
1000
1500
2000
2500
3000
0.0 0.1 0.2 0.3 0.4 0.5 0.6 0.7 0.8
Te
mp
era
ture
(°C
)
Radial Distance (cm)
Design 5
Reference CANDU
EnrichedRegion
DepletedRegion
Fuel Centreline
UO2 Melting Point
U-Metal Melting Point
Page | 113
4.4 Mass and Activities of Molybdenum-99
The proposed designs utilize 19.5 wt% U-235 enriched fuel over several target
pins which can generate a large yield of Mo-99 per bundle. Tasks 1, 2 and 3 ensure that
high yields of Mo-99 can be done without significantly changing the bundle physics and
fuel safety characteristics.
The mass and activity of Mo-99 is calculated for each design by extension of the
DRAGON calculated fission rates as described in Section 3.4.3. The total Mo-99
production values are 2335, 2297, 2336, 4131 and 4268 six-day Curies for Design 1 to 5,
respectively. This yield corresponds to approximately 19% of the world weekly demand
for Designs 1, 2 and 3, and approximately 34% of the world weekly demand for Designs 4
and 5.
The activities of Mo-99 produced per bundle at EOB and six-day Curies are listed
in Tables 4-26 through 4-30. The required extraction rate to meet worldwide demands
of Mo-99 for each design is also specified. A production cycle of 6 bundles per week for
Designs 1, 2 and 3, or 3 bundles per week for Designs 4 and 5 would yield sufficient
quantities of Mo-99 to ensure stable supply of Mo-99 to satisfy the global demand.
Page | 114
Table 4-26: Design 1 Molybdenum-99 Production Results
Bundle Location
EOB Activity of Mo-99 (Ci)
Total EOB Activity of Mo-99
Total EOB Mass of Mo-99
Total Six-Day Curies of Mo-99
Weekly Extraction Rate Required to Meet Worldwide Demand
Ring 1 0 15006 Ci/Bundle
31.26 mg/Bundle
2335 Ci/Bundle
~6 Bundles/Week
Ring 2 0 Ring 3 0 Ring 4 15006
Table 4-27: Design 2 Molybdenum-99 Production Results
Bundle Location
EOB Activity of Mo-99 (Ci)
Total EOB Activity of Mo-99
Total EOB Mass of Mo-99
Total Six-Day Curies of Mo-99
Weekly Extraction Rate Required to Meet Worldwide Demand
Ring 1 0 14761 Ci/Bundle
30.74 mg/Bundle
2297 Ci/Bundle
~6 Bundles/Week
Ring 2 0 Ring 3 0 Ring 4 14761
Table 4-28: Design 3 Molybdenum-99 Production Results
Bundle Location
EOB Activity of Mo-99 (Ci)
Total EOB Activity of Mo-99
Total EOB Mass of Mo-99
Total Six-Day Curies of Mo-99
Weekly Extraction Rate Required to Meet Worldwide Demand
Ring 1 0 15008.21 Ci/Bundle
31.26 mg/Bundle
2336 Ci/Bundle
~6 Bundles/Week
Ring 2 0 Ring 3 0 Ring 4 15008
Page | 115
Table 4-29: Design 4 Molybdenum-99 Production Results
Bundle Location
EOB Activity of Mo-99 (Ci)
Total EOB Activity of Mo-99
Total EOB Mass of Mo-99
Total Six-Day Curies of Mo-99
Weekly Extraction Rate Required to Meet Worldwide Demand
Ring 1 551.8 26547 Ci/Bundle
55.29 mg/Bundle
4131 Ci/Bundle
~3 Bundles/Week
Ring 2 3470 Ring 3 7894 Ring 4 14629
Table 4-30: Design 5 Molybdenum-99 Production Results
Bundle Location
EOB Activity of Mo-99 (Ci)
Total EOB Activity of Mo-99
Total EOB Mass of Mo-99
Total Six-Day Curies of Mo-99
Weekly Extraction Rate Required to Meet Worldwide Demand
Ring 1 583.0 27423 Ci/Bundle
57.11 mg/Bundle
4268 Ci/Bundle
~3 Bundles/Week
Ring 2 3606 Ring 3 8192 Ring 4 15040
Page | 116
Although the centre and middle rings provide higher margins to heating limits as
depicted in Figures 4-8 through 4-12, the 4th ring provides a higher flux exposure which
is a key factor for the production of Mo-99. This aspect of core neutronics is utilized in
Designs 1, 2 and 3. Furthermore, by only using the outer most rings for Mo-99
production, the post processing procedure becomes simpler since only those pins will
need to be demounted for processing, and can easily be replaced with fresh Mo-99
targets for another production run. Ideally the re-use of the remaining pins should be
limited to a few cycles since excessive irradiation of the NU will produce Pu-239 through
neutron absorption. Build-up of small amounts of Pu-239 will also occur in the depleted
fuel inside the Mo-99 producing pins. However, due to the 20-day irradiation period and
the presence of only a small number Mo-99 producing bundles in the core, the effect of
Pu-239 build-up on the overall reactivity is expected to be small.
The production of Mo-99 must be balanced against the bundle power and linear
heating limits. Assessment of Designs 1, 2 and 3 showed that the bundle reactivity and
distribution of power resembles greatly with the standard CANDU bundle at the pin
level. This resemblance made it possible to extend the design of the 4th ring elements to
other rings for maximum Mo-99 yield. Tables 4-26 through 4-30 list the total six-day
Curies of Mo-99 produced for each design. As calculated in these tables, Designs 4 and 5
distribute the total power of the bundle over increased number of target elements, 37
pins in total, and therefore provide a much higher yield of Mo-99 compared to Designs 1,
2 and 3.
Page | 117
Chapter 5
Concluding Remarks and Future Work
This thesis explores the possibility of using modified 37-element fuel bundles for
the production of Mo-99 in existing CANDU reactors without affecting the core
properties or day-to-day operations of the plant. The tasks performed in Sections 4.1,
4.2 and 4.3 are used to evaluate the viability of the designs with respect to the existing
safety margins as well as to demonstrate the similarity of the proposed target bundles
to the standard 37 element bundle behavior.
As mentioned above, various designs with different amounts of 19.5 wt% U-235
enriched fuel were simulated using the DRAGON lattice code and the fresh fuel kinf values
were recorded for each case. The use of 19.5 wt% U-235 enriched fuel as Mo-99 targets
in different rings of a 37-element fuel bundle result in increased fission rates and hence
power rating of the enriched region is increased. In order to have a high confidence in
the available margins to the maximum linear power ratings and centreline temperature
limits, the bundles are assumed be irradiated in the highest power channel of the CANDU
reactor core corresponding to the maximum instantaneous power of 900 kWth.
In conclusion, the design of modified fuel bundles for Mo-99 production met the
criteria specified in Section 3.1 of this thesis. Although the impacts of the enriched target
pins on safety analysis were not directly examined in this work, the similarity in the
unitcell eigenvalue (kinf) and the pin linear heat rating with the reference CANDU bundle
suggest that the resultant impact on accident analysis should be small. However, direct
Page | 118
confirmation may still be required before the new design can be implemented in
operating reactors.
Over the last few years, there have been a number of supply shortages of Mo-99.
The situation is to deteriorate further with the expected permanent shutdown of the
Canadian NRU reactor in 2016. The CANDU power reactors can play a large role in
ensuring a stable supply of Mo-99. The feasibility of producing large and continuous
quantities of Mo-99 in the CANDU power reactors has been demonstrated in this thesis.
The continuous and reliable supply of medical isotopes will ensure the availability of life-
saving medical procedures for millions of patients around the globe.
Recommendations for Future Work:
During the course of this research, some areas were identified as requiring future
study if the production of medical isotopes using one of the proposed bundle designs in
CANDU reactor was actually begun. These areas of potential research include:
Fuel pellet manufacturability: Designs 2, 3, 4 and 5 proposed in this thesis have
very thin annular enriched fuel regions composed of either UO2 or U-metal on the
periphery of the fuel pellet. Although the new fuel manufacturing methods have
significantly advanced, the proposed thin layers may still challenge manufacturing
feasibility. The manufacturability of the posed fuel pellets should be examined.
Use of demountable fuel bundles: The study assumes the use of demountable
bundles for the proposed designs. Upon completion of the irradiation cycle, the target
pins will be demounted and sent for processing. Although, this is not critical to the
Page | 119
proposed study, it will provide ease with respect to fuel reprocessing and reuse. The
feasibility of demountable bundles to use in the operating CANDU reactors should be
examined.
Handling and processing of medical isotopes producing 37-element bundle: Upon
extraction from the reactor the pins with enriched uranium will be sent to the Mo-99
production facilities for further processing, whereas the remaining pins can either be
sent away to spent fuel storage or be mounted on another target fuel bundle and
reloaded into the reactor for another Mo-99 production cycle. Additional fuel handling
procedures would need to be developed to remove the Mo-99 target pins from the
demountable bundle and send them for processing. Handling and processing of newly
designed fuel bundles would require updating the existing infrastructure and is a subject
for future research.
Pilot production: The study assumes that the proposed bundle will be irradiated
in the highest power channel of the CANDU reactor. The 900 kWth bundle power is the
upper limit for a typical CANDU fuel bundle and the bundle power at the periphery
location can be half of this value [50]. Ideally the new bundles will be first irradiated in
a low-power channel on the periphery of the core to get more operational experience
before moving the bundles to the high-power central channels. Therefore, from an
operational standpoint, it is advisable to load the new proposed bundles in the periphery
channels first to gain operational experience before loading them into the high power
channels of the CANDU core.
Page | 120
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Appendices
Appendix A – Potential Producers of Reactor Produced
Molybdenum-99
Numerous projects have surfaced worldwide related to the building of new
reactors dedicated to the Mo-99 production, including production of Mo-99 from an
existing facility that was not originally built for that purpose. In some cases, these
initiatives are expected to play a big role in the production of medical isotopes in the
future, while in other cases, the projects are either cancelled or lobbying for
governments to provide support for further research to be carried out.
The following is a list of potential producers of reactor-based Mo-99 that have the
technological resources to play a large role in the production of medical isotopes in the
future.
A.1 Multipurpose Applied Physics Lattice Experiment (MAPLE)
Designed by Atomic Energy of Canada Limited (AECL), two reactors, MAPLE I and
II were planned and constructed to supply the world’s demand for Mo-99. The MAPLE
reactors were designed to generate 10 MW of heat for the sole purpose of medical
isotope production [51]. Each reactor was capable of producing enough medical
isotopes to supply 100% of the worldwide demand (~12000 six-day Curies per week).
The MAPLE reactors were planned to use LEU fuel and HEU targets.
Page | 136
Designed and built to replace the 54 year old NRU reactor in Canada, the project
was estimated to cost $140 million but ended up costing much more due technical design
flaws which were discovered during commissioning. It was discovered that these
reactors have a positive power coefficient of reactivity. The reactors were designed to
have a small negative power coefficient of reactivity, estimated at -0.12 mk/MW, but it
was measured to be +0.28 mk/MW.
The power coefficient of reactivity describes the number of neutrons available
per generation per unit change in power. A positive value indicates that there are more
neutrons available in each subsequent generation as the reactor power is increased. This
meant that the reactor inherently tried to increase the power during power increases, a
positive feedback. The original safety systems of the reactor were inadequate and design
changes were implemented to accommodate the positive power coefficient of reactivity.
Investigations by AECL and other contracted service providers were unable to explain
the positive power coefficient, and in 2008, AECL and the Government of Canada
announced that the project would be discontinued [52].
There has been much debate among experts on the issue of reviving the MAPLE
reactors. A number of scientists believe that the reactor could have operated safety with
a positive power coefficient of reactivity, after the design changes to take it into account
were implemented. However, another roadblock hindering the MAPLE project was that
the fuel processing facility was designed to accommodate HEU targets. Conversion to
LEU targets would have required a significant redesign of the processing facility with
Page | 137
larger waste tanks, etc. Calls to complete commissioning of the MAPLE project have not
received much attention.
It is expected that a general re-revisit of the positive power reactivity coefficient
problem may take up to 6 years to rectify if possible. If it is later decided that redesigning
and replacing the entire core of MAPLE reactors is the only way to solve the positive
power reactivity coefficient problem, those efforts may take additional 7 to 10 years and
may cost tens of millions of dollars [53].
A.2 Aqueous Homogeneous Reactor (AHR)
Babcock & Wilcox (B&W) have proposed to build an aqueous homogeneous
reactor (AHR), also known as a solution reactor, which will utilize an LEU fuel salt
dissolved in acid and water. In this reactor, the uranium in the solution is both the
reactor fuel and the target material. This system would eliminate the need to
manufacture or encapsulate a target, and un-fissioned uranium can be recycled back into
the reactor instead of being removed as waste. Various solution forms of fuel are
possible, such as: uranyl nitrate (UO2(NO3)2), uranyl sulfate (UO2SO4), or uranyl fluoride
(UO2F2) [54]. The extraction process itself would not differ remarkably from the existing
adsorption process of using an alumina column that is currently used by processing
facilities.
B&W has estimated that an AHR reactor could generate approximately 18% of
the North American Mo-99 demand (1100 six-day Curies per week) while assuming a 26
Page | 138
hour processing time. The proposal suggests building three to four 200 kW units for
higher Mo-99 yields. They have also projected a total waste volume of less than 5 m3
each year consisting generally of alumina column wastes [54].
B&W assumes that five years will be required from conceptual design (which has
begun) to commercial operation for their newly designed AHR. However, the plan is still
lacking concrete budget projections derived from actual experience from building
solution reactors. B&W’s own initial estimate states that less than $100 million will be
required for research and development of the AHR [55].
Being first of its kind in terms of design and scale, another hurdle to the
construction of AHR is lack of regulatory framework. Current nuclear reactor
regulations do not specifically address AHR, so licensing under current regulations may
require clarifications, or new regulations may be needed to appropriately address the
safety of the solution reactors [55].
A.3 Open Pool Australian Light-Water (OPAL) Reactor
The OPAL reactor started its operation in late 2006. This multipurpose pool type
reactor was built by INVAP for the Australian Nuclear Science and Technology
Organization (ANSTO). The purpose was to replace the aging High Flux Australian
Reactor.
Page | 139
OPAL is a 20 MW reactor with peak thermal neutron flux: 3x1014 n·cm-2·s-1 in the
reflector vessel. The core of OPAL consists of compact 16 uranium oxide fuel assemblies
interspersed with control rods. The fuel assemblies are cooled by demineralised light
water, while the core is surrounded by heavy water moderator in a zirconium alloy
reflector vessel at the bottom of a 13-metre-deep open pool of light water [56].
OPAL uses LEU fuel with around 20% U-235 enrichment by weight [56]. This
gives OPAL a distinct advantage over other research reactors around the world in terms
of nuclear security and safeguards. OPAL has the capacity to operate 340 days a year
which is a significant increase over the operating levels typically achieved by comparable
research facilities.
The ANSTO facility includes an onsite processing facility which produces many
important radionuclides, such as Mo-99, extracted from LEU uranium-aluminium alloy
targets. The processing facility was also build by INVAP with a budget of $200 Million
[57]. The facility supplies medical isotopes to meet 100% of Australia’s demand, as well
as the demands of a number of overseas countries, especially in the Asia-Pacific region.
The reactor has been producing medical isotopes since May 2008, and is expected to
produce medical isotopes for the next 40 years.
The reactor is currently producing Mo-99 one manufacturing run per week. If
there is a need to produce for the wider market, such as North America, the
manufacturing process can be run multiple times per week with multiple targets being
irradiated [55]. However, before the operators of OPAL decide on expanding their
manufacturing runs, appropriate approvals by the government drug oversight agencies
Page | 140
will be required in order to use Mo-99 made by ANSTO. In July 2006, the US Food and
Drug Administration (FDA) and Health Canada authorized Lantheus Medical Imaging to
use Mo-99 produced by the OPAL reactor to make Tc-99m for diagnostic imaging for
North American health care facilities ([53], [58]).
Beside some political and long-distance transportation related issues, the OPAL
reactor was intended to only provide medical isotopes for the local Australian and New
Zealand markets, and is only capable of providing a small fraction of the worldwide
demand of Mo-99 ([53], [55]).
A.4 Jules Horowitz Reactor (RJH)
Jules Horowitz Reactor is a 100 MW material test reactor located at the Cadarache
site in southern France. Built by the French Commissariat à l'énergie atomique (Atomic
Energy Commission, CEA), the reactor is expected to replace the 70 MW OSIRIS reactor
when the RJH becomes operational. The reactor is projected to be operational in the
second quarter of 2016, with an estimated budget of 500 million Euros and with a
lifetime of 50 years ([59], [60]).
The RJH reactor core is dismountable type. Reactor fuel is inserted in the form of
cylinders of six concentric curved fuel plates hot-rolled from uranium alloys. 46
cylinders can fit in the one-piece aluminum alloy core rack at a time. The fuel is enriched
to 25% U-235 by weight, amounting to a total mass of 21 kg U-235. The dismountable
reactor core is partly surrounded by a beryllium reflector. The reactor core between
Page | 141
coolant inlet and outlet can be replaced to accommodate scope of future research
initiatives [60].
Although the facility and the related infrastructure was initially conceptualized
for scientific studies dealing with material and fuel behaviour under irradiation, a recent
focus on the production of medical isotopes as part of the European strategy to ensure
reliable supply for use in nuclear medicine has been gaining some momentum ([61],
[62]). The plan is to coordinate the production with the isotopes processing facilities in
the Netherlands to provide a back-up supply for medical isotopes for Europe.
RJH will have a thermal neutron flux of 5x1014 n·cm-2·s-1 in the reflector region
[63]. The reactor is expected to be operational for 220 days a year and can have flexible
Mo-99 production cycles. RJH is expected to produce 25% (1200 six-day Curies per
week) of the European base needs, with the possibility to increase the production up to
50% of European needs (2400 six-day Curies per week) if required. This can be achieved
by irradiating 32 to 48 LEU targets in the core and in the reflectors in both fixed and
movable positions [61].
Design studies for Mo-99 irradiation systems based on LEU targets has been
completed, and the irradiation tests of LEU targets are expected to take place in the
second quarter of 2018. The reactor is expected to begin its normal level of Mo-99
production in 2019 [62].
The RJH has the capacity to increase the number of target irradiation in order to
significantly contribute to the Mo-99 world market. However, the reactor is built mainly
Page | 142
for material testing purposes and is not likely to limit its activity to the production of
Mo-99 [64]. The project is expected to supply a fraction of the European medical isotope
need and is unlikely to play a major role in the North American medical isotope market.
A.5 China Advanced Research Reactor (CARR)
The China Advanced Research Reactor began its construction on August 26, 2002
and on March 1st, 2012 it successfully achieved full power operations ([65], [66]). The
reactor is located at the China Institute of Atomic Energy Fangshan, Beijing site. The
sophisticated light-water tank type reactor with a heavy water reflector is one of the
most advanced research reactors in the world, producing 60 MW at full power [66]. The
core of CARR is immersed in a 15-meter pool of water. CARR has maximum thermal
neutron flux of 1×1015 n·cm-2·s-1 at the centre of the reactor core, and about
8×1014 n·cm-2·s-1 at the heavy water reflector. CARR has nine tangent horizontal neutron
beam channels available for experiments and 25 vertical irradiation channels [67].
The overall design objective of CARR is to enhance China’s research capabilities
in fields such as nuclear physics and chemistry, neutron scattering experiments, testing
of reactor materials and nuclear fuels and neutron activation analysis. The reactor is
also being used to irradiate targets for the production of radioactive isotopes [65].
Mo-99 produced in CARR is sent to CIRA member companies for processing and
to produce Tc-99m generators. The CARR production capacity per week is about 250
six-day Curies of Mo-99. The demand activities of Mo-99 in China are 200 six-day Curies
Page | 143
per week. Therefore, CARR is expected to supply 100% of the China’s and neighbouring
countries medical isotope needs and is unlikely to play a major role in the North
American medical isotope market.
A.6 University of Missouri Research Reactor Center (MURR)
Built in 1966, the University of Missouri Research Reactor is a 10 MW tank type
reactor. MURR is the largest university research reactor in North America. It is a flux-
trap reactor with high intensity thermal and fast neutron flux which can be as great as
5x1014 n·cm-2·s-1 [68]. The reactor runs 24 hours a day, 7 days a week, with a scheduled
12 hour maintenance shutdown on Mondays. In 2006, the reactor was relicensed to
operate for another 20 years. The MURR is attempting to establish a domestic
production source of Mo-99. In 2007, the facility produced 41 different isotopes, and
more than 1000 shipments were exported to 14 different countries [69].
MURR has indicated its intention to commercially produce Mo-99 and is soliciting
funding for studying the design and construction of the processing facilities for post
irradiation extraction of medical isotopes [70]. Overall, the objective is to develop the
capability to produce Mo-99 from LEU targets, with little change to the current reactor
layout.
MURR has completed a conceptual design of a processing facility which will allow
the safe processing of the LEU targets. The facility is to be located adjacent to MURR to
permit safe transfer of targets to the facility after irradiation. Production objectives are
Page | 144
to produce 50% of current U.S. weekly demand (3000 six-day Curies per week) [71].
MURR could also help to fill gaps for up to about 75% of the US demand when other
reactors are on planned shutdowns. This can be achieved through short-term shifts in
production schedules [70]. It is estimated that it will take 3-4 years for MURR to build
the appropriate processing facilities to handle the anticipated volumes of Mo-99 [53].
The current status of the planned upgrades is unknown.
In March 2011, MURR entered into a contract with NorthStar to build an electron
linear accelerator to produce low specific activity Mo-99. The goal is to ramp up the
production to 3000 six-day Curies per week, but have only been able to produce just over
1100 six-day Curies ([72], [73]). Although the separation chemistry of the accelerator
produced low specific activity of Mo-99 is very well understood, the generated doses do
not fit in the current distribution stream. The low specific activity of Mo-99 requires new
generating systems to utilize the products and generate Tc-99m in activity
concentrations typically needed in nuclear pharmacies [73].
A.7 Sandia National Laboratories (SNL)
Home to the Annular Core Research Reactor (ACRR), the Sandia National
Laboratories are located on Kirtland Air Force Base in Albuquerque, New Mexico and are
managed and operated by the Sandia Corporation, which is a wholly owned subsidiary
of Lockheed Martin Corporation. Since the late 1990s, SNL has been seeking for licensing
approval to produce Mo-99. The initial preparatory work included reproduction and
Page | 145
verification of the Cintichem Mo-99 production process, development of production
hardware, modification of the hot cell facility, reconfiguration of the ACRR and
preparation of documentation to meet FDA and US-NRC approvals [74].
The ACRR is an open tank-type reactor filled with about 10 meters of water which
provides both core cooling and radiation shielding. Heat is transferred to the open water
pool through natural convection. The pool itself is cooled by an external heat exchanger.
The core of ACRR consists of an annular array of UO2-BeO fuel elements. The height of
the active fuel part is 52 centimetres. For target irradiation, the dry steel-lined control
cavity can be removed from the centre of the core to provide a water-filled region. Two
options are available for target irradiation, one with a maximum of 19 targets and the
other with a maximum of 37 targets at a time. With targets inserted, only 180 or 130
conventional fuel assemblies, depending on the option selected, would be required to
operate the reactor [75]. ACRR has flexibility to operate at 30000 MW in pulse mode or
4 MW in a steady state mode [55].
The SNL site which includes ACRR, hot cell facility, and other associated facilities
are a promising option for the isotope production program. The characteristics of ACRR
are fully compatible with radioisotope production. It is capable of being dedicated to
continuous isotope production, which is necessary to meet the demands for Mo-99. The
connected hot cell facility was modified in the 1990s for Mo-99 production. The ACRR
site is in proximity to excellent air transportation facilities which are useful for
radioisotope shipments [76].
Page | 146
The SNL facility has the capability to serve as a backup supply to provide up to
30 % of the U.S. market demand (~1800 six-day Curies per week) under normal
circumstances. It also has the capability to produce 100% of US Mo-99 requirement
(~6000 six-day Curies) should the need arise [75]. The problem however, is that the
reactor is currently being used by the defense programs group at the US-DOE. In order
to free the ACRR for production of medical radionuclides, it would require DOE to
reassign the mission of the ACRR from defense program uses, and make significant
investments in the reactor and the processing facilities [55].
It is estimated that it would require $10 to $50 million to convert the ACRR into
a steady state reactor and make necessary upgrades to the existing hot cell facility in
order to process Mo-99 using LEU targets [55]. Furthermore, the current fuel is 35%
enriched U-235, which is considered HEU. However, it is possible to convert the ACRR
to use LEU fuel for the production of Mo-99.
The proposed Mo-99 project regarding changing the mission of the ACRR for
Mo-99 production has been dropped by the DOE in favour of a new LEU reactor for the
production of Mo-99 at SNL. In the more recent publication coming out of SNL, the
facility is proposing to build a new reactor for the sole purpose of producing medical
isotopes alongside a hot cell facility ([77], [78] [79], [80]). The intention is to construct
a new reactor which is capable of producing 100% of the U.S demand (~6000 six-day
Curies per week). The reactor concept is unique in that the fuel for the reactor and the
targets for the Mo-99 production are the same. In other words, no driver core is required
for irradiation of Mo-99 targets. The fuel pins will be irradiated on a 7 to 21 day cycle.
Page | 147
The reactor will use LEU uranium oxide fuel enriched to 20 wt% of U-235. The fuel pins
will be approximately 1 cm in diameter and 30 to 40 cm in height, encapsulated in a
zirconium alloy cladding. An estimated 90 to 150 fuel pins will be arranged in the core
located inside a water pool about 9 meters deep [77].
The reactor power level will be between approximately 2 MW. Since the
production of 6000 six-day Curies per week requires at least 1.1 MW of continuous
target fission power, assuming two post-irradiation days for processing and shipping
[77], the proposed reactor is capable of meeting 100% of North American demand. The
proposed facility will also have an adjacent hot cell facility which would be connected to
the reactor pool by a water channel to facilitate remote transfer of irradiated targets for
processing. Processing will be done using oxide dissolution and separation processes. A
provisional patent for the SNL medical isotope reactor concept was filed on
September 11, 2009 [77].
Although, there are no impediments to prevent the SNL medical isotope reactor
concept along with its hot cell facility, from being designed, fabricated, and licensed
today, the only question is who will be funding this project. A report by US Society of
Nuclear Medicine (SNM) task group suggests that SNL should explore the possibility of
partnerships with National Nuclear Security Administration and DOE [55].
Page | 148
A.8 Other Potential Suppliers of Reactor Produced Molybdenum-99
Following the major disruptions in the supply of medical isotopes in 2007, the
Canadian government has initiated OECD12 meetings on radioisotope availability in Paris
and again in Toronto in 2009. Also in efforts to expand Canada's isotope production
capabilities, in May 2009 the provincial and federal governments announced a $22-
million fund for the McMaster University research reactor to upgrade the research
reactor’s infrastructure. However, the McMaster Nuclear Reactor (MNR) is a 50-year-
old reactor and will use HEU targets [53]. According to a report by SNM, even with 24/7
operation, it is estimated that MNR can only supply about 30% of North American Mo-99
demands [55]. The MNR is likely to assume the role of a backup supplier rather than a
primary producer of Mo-99 for North America.
In the United States, a proposal to produce Mo-99 by using LEU solution targets
at the University of California at Davis in the McClellan Nuclear Radiation Center reactor
could also reach the commercial production stage in 3-4 years [53].
Table A-1 provides a list of many potential reactor projects at various stages of
development. Some of these projects are very well advanced, while others are still in
proposal or a design phase seeking funding and/or regulatory approvals before actually
advancing to the construction phase.
12 The Organisation for Economic Co-operation and Development
Page | 149
Table A-1: Potential Future Suppliers of Reactor Produced Molybdenum-99
[13]
Reactor Facility
Target Expected Normal Capacity per Week (six-day Curies)
Estimated First Full Year of Production
Status
MNR (McMaster University, Canada)
LEU 1500 Project is seeking funding.
RIAR (Russian Federation)
HEU 800-2000 2015 The facility includes three reactors. Two of which will produce Mo-99, with the third being a back-up. Currently in Phase 2 of development.
INR, Pitesti (Romania)
LEU 900 2015 Proposal
FRM-II (Germany)
LEU 1950 2016 Pending LEU target design approval.
Coqui (United States)
LEU 7000 2017 Project is seeking funding.
BMR (Brazil) LEU 1000 2018 Project is in preliminary design stage.
RA-10 (Argentina)
LEU 200 2019 Project is in preliminary design stage.
PALLAS (Netherlands)
LEU 7300 2023 Project is in preliminary design stage. Project is also seeking funding.
SAFARI-II (South Africa)
LEU 3000 2026 Feasibility study for this project is underway.
Page | 150
A.9 New Approaches in Diagnostic Nuclear Medicine
Going into the future, there may be a number of accelerators and nuclear-based
technologies that could play a potential role in providing a stable supply of Mo-99. In
addition, there are a variety of new and emerging medical imaging techniques that could
possibly bypass the need for nuclear reactor based medical isotopes. Positron Emission
Tomography – Computed Tomography has already been successful in this regard.
However, there is no guarantee that any new technology will receive clinical acceptance
even though it may be commercially viable. Cost, ease of use, facilities for the production
and transportation may be some of the determinants [81].
Other means of producing Mo-99 include photo-fission of U-235, neutron
activation of Mo-98, and photo neutron interactions of Mo-100. Even before the 2007
crisis, TRIUMF based in Vancouver, Canada, proposed a plan to produce Mo-99 by
photon fission of U-238 by using photons from an electron accelerator [82]. This method
of production yields low quantities of Mo-99, which requires multiple units to supply the
world's demands.
Construction of new reactors or conversion of existing reactors as well as
possible use of accelerators to meet increasing demands has been the focus of the
medical isotope industry in recent years, including the use of alternate radionuclides and
medical imaging techniques ([2], [8], [11], [81], [83], [84]).
Page | 151
Appendix B – Materials, Lattice Specifications and Important
Parameters for 37-Element CANDU Fuel Bundle Calculations
Materials, Lattice Specifications and Other Important Parameters
Value
Initial Uranium Composition Natural UO2 U-235 U-238 Enriched UO2/U-metal U-235 U-238 Depleted UO2/U-metal U-235 U-238
Weight Percentage 0.711% 99.289% 19.50% 80.50% 0.200% 99.8%
UO2 fuel density U-metal fuel density
10.60 g/cm3 18.95 g/cm3
Fuel temperature 1155 K Element radius U-metal fuel element radius
0.6075 cm 0.4266 cm
Element length/bundle length 49.53 cm Number of fuel pins 37 Inner fuel ring radius (6) Middle fuel ring radius (12) Outer fuel ring radius (18)
1.4885 cm 2.8755 cm 4.3305 cm
Cladding material Cladding radius
Zircaloy 0.6540 cm
Pressure tube Inner radius Outer radius
5.1689 cm 5.6032
Calandria tube Inner radius Outer radius
Zircaloy 6.4478 cm 6.5875 cm
Coolant Atom purity Density Temperature
D2O 99.75 % 0.8360 g/cm3 549 K
Moderator Atom purity Density Temperature
D2O 99.91 % 1.083 g/cm3 346 K
Page | 152
Fuel channel square pitch 28.575 cm Approximate burnup 906.62 MWd/MgU Mo-99 fraction in fission products 6.1% Mo-99 decay constant (λ) 0.252 d-1
Mo-99 atomic weight 99.91 g/mol
Page | 153
Appendix C – Initial Estimates of Enriched Fuel Region Thickness and
Pin Radius for UO2 and U-Metal Fuel Designs Based on Uranium Mass
Balancing
Design 1
Fuel Pellet Radius = Rf = 0.6075cm
Fuel pin length = Lf = 49.5cm
Assumptions:
The isotopic composition of Uranium includes only U-235 and U-238 isotopes. Other uranium isotopes (U-234, U-236, etc.) are ignored.
Weight percentage of U-235 in natural uranium, rnat,U = 0.71% Weight percentage of U-235 in enriched uranium, renr,U = 19.5% Weight percentage of U-235 in depleted uranium, rdep,U = 0.2% Density of UO2 will remain the same irrespective of the enrichment, ρnat,U = ρdep,U = ρenr,U
= 10.6 g/cm3
Atomic weight of enriched Uranium, MU, is:
238
235
235
235
238
238
235
235 11
U
U
U
U
U
U
U
U
U M
r
M
r
M
r
M
r
M
Atomic weight of UO2 = 16*2 OU MM , therefore:
Mass of U-235 in CANDU-6 fuel pin is:
mnat,U-235 = Unat
OnatU
natUUnatff r
MM
MLR ,
16
,
2
*2
Mass of U-238 in CANDU-6 fuel pin is:
mnat,U-238 = )1(*2
,
16
,
2
Unat
OnatU
natUUnatff r
MM
MLR
In Design 1, the enriched UO2 fuel region is inscribed inside the depleted uranium annulus. The mass of U-235 in the enriched fuel pin is therefore:
m’enr,U-235 = Uenr
OenrU
enrUUenrfenrf r
MM
MLR ,
16
,
2
*2'
Page | 154
The mass of U-235 in depleted uranium annulus is:
m’dep,U-235 = Udep
OdepU
depU
Udepfenrff rMM
MLRR ,
16
,
22
*2)'(
To calculate the radius of the enriched fuel layer in Design 1, a simple mass balance relation can be formulated based on the mass of U-235 in the reference CANDU-6 and Design 1 fuel pins.
mnat,U-235 = m’enr, U-235 + m’dep, U-235
Udep
OdepU
depU
Udepfenrff
Uenr
OenrU
enrUUenrfenrfUnat
OnatU
natUUnatff
rMM
MLRR
rMM
MLRr
MM
MLR
,
16
,
22
,
16
,
2
,
16
,
2
*2)'(
*2'
*2
The above equation can be simplified to:
UdepUdepUdepenrffUenrUenrUenrenrfUnatUnatUnatf rRRrRrR ,,,
22
,,,
2
,,,
2 )'('
UnatUnatUnatfUdepUdepUdepf
UenrUenrUenrenrfUdepUdepUdepenrf
rRrR
rRrR
,,,
2
,,,
2
,,,
2
,,,
2 ''
(i)
where,
16
1
238
,
235
,
1
238
,
235
,
16
,
*21
1
*2
O
U
Unat
U
Unat
U
Unat
U
Unat
OnatU
natUUnat
MM
r
M
r
M
r
M
r
MM
M
16
1
238
,
235
,
1
238
,
235
,
16
,
*21
1
*2
O
U
Udep
U
Udep
U
Udep
U
Udep
OdepU
depU
Udep
MM
r
M
r
M
r
M
r
MM
M
16
1
238
,
235
,
1
238
,
235
,
16
,
*21
1
*2
O
U
Uenr
U
Uenr
U
Uenr
U
Uenr
OenrU
enrUUenr
MM
r
M
r
M
r
M
r
MM
M
Eq. (i) then becomes:
Page | 155
UenrUenrUenrUdepUdepUdep
UnatUnatUnatUdepUdepUdepf
enrfrr
rrRR
,,,,,,
,,,,,,
2
2
UenrUenrUenrUdepUdepUdep
UnatUnatUnatUdepUdepUdepf
enrfrr
rrRR
,,,,,,
,,,,,,
2
(ii)
Assuming the densities do not change for different enrichments:
UnatUdepUenr ,,,
Eq. (ii) can be simplified to:
UenrUenrUdepUdep
UnatUnatUdepUdepf
enrfrr
rrRR
,,,,
,,,,
2
where,
994.15*2051.238
%71.01
044.235
%71.0
051.238
%71.01
044.235
%71.0
*21
1
1
1
16
1
238
,
235
,
1
238
,
235
,
,
O
U
Unat
U
Unat
U
Unat
U
Unat
Unat
MM
r
M
r
M
r
M
r
8815.0, Unat
994.15*2051.238
%2.01
044.235
%2.0
051.238
%2.01
044.235
%2.0
*21
1
1
1
16
1
238
,
235
,
1
238
,
235
,
,
O
U
Udep
U
Udep
U
Udep
U
Udep
Udep
MM
r
M
r
M
r
M
r
8815.0, Udep
994.15*2051.238
%5.191
044.235
%5.19
051.238
%5.191
044.235
%5.19
*21
1
1
1
16
1
238
,
235
,
1
238
,
235
,
,
O
U
Uenr
U
Uenr
U
Uenr
U
Uenr
Uenr
MM
r
M
r
M
r
M
r
8813.0, Uenr
Page | 156
Therefore,
195.0*881.0002.0*882.0
0071.0*882.0002.0*882.06075.0 2
enrfR
Design 2
In Design 2, the depleted UO2 fuel region is inscribed inside a thin enriched fuel annulus. The mass of U-235 in the depleted uranium pin is:
mdep,U-235 = Udep
OdepU
depU
Udepfdepf rMM
MLR ,
16
,
2
*2
The mass of U-235 in the enriched fuel annulus is:
menr,U-235 = Uenr
OenrU
enrUUenrfdepff r
MM
MLRR ,
16
,
22
*2)(
Again, to calculate the thickness of the thin enriched fuel layer in Design 2, a simple mass balance relation can be formulated based on the mass of U-235 in the reference CANDU-6 and Design 2 fuel pins.
mnat,U-235 = mdep, U-235 + menr, U-235
Uenr
OenrU
enrUUenrfdepff
Udep
OdepU
depU
UdepfdepfUnat
OnatU
natUUnatff
rMM
MLRR
rMM
MLRr
MM
MLR
,
16
,
22
,
16
,
2
,
16
,
2
*2)(
*2*2
Based on the previous terminology for Aenr,U, Adep,U and Anat,U, the above equation can be simplified
to:
UenrUenrUenrfdepffUdepUdepUdepfdepfUnatUnatUnatff rLRRrLRrLR ,,,
22
,,,
2
,,,
2 )(
UenrUenrUenrdepffUdepUdepUdepdepfUnatUnatUnatf rRRrRrR ,,,
22
,,,
2
,,,
2 )(
UnatUnatUnatfUenrUenrUenrfUdepUdepUdepdepfUenrUenrUenrdepf rRrRrRrR ,,,
2
,,,
2
,,,
2
,,,
2
Renrf = 0.098 cm ≅ 0.1 cm
Page | 157
Separating Rdepf to one side gives:
UdepUdepUdepUenrUenrUenr
UnatUnatUnatUenrUenrUenrf
depfrr
rrRR
,,,,,,
,,,,,,
2
2
UdepUdepUdepUenrUenrUenr
UnatUnatUnatUenrUenrUenrf
depfrr
rrRR
,,,,,,
,,,,,,
2
(iii)
Again, assuming the densities do not change for different enrichments:
UnatUdepUenr ,,,
Eq. (iii) simplifies to:
UdepUdepUenrUenr
UnatUnatUenrUenrf
depfrr
rrRR
,,,,
,,,,
2
Evaluating the above equation gives:
002.0*8815.0195.0*8813.0
0071.0*8815.0195.0*8813.06075.0 22
cmRdepf
cmcmRdepf 600.05994.0
Thickness of the enriched layer then becomes:
Design 3
Assumptions:
Density of uranium metal, ρdep,U = ρenr,U = 18.95 g/cm3
In Design 3, the depleted U-metal fuel region is inscribed inside a thin enriched U-metal fuel annulus. Furthermore, uranium metal is used in the modified fuel bundle for both depleted and enriched regions. The mass of U-235 in the depleted uranium pin is:
tenrf =0.6075 cm – 0.6 cm = 0.0075 cm
Page | 158
mdep,U-235 = Udep
depU
depU
Udepfdepf rM
MLR ,,
2
The mass U-238 in the depleted uranium pin is:
mdep,U-238 = )1( ,,
2
Udep
depU
depU
Udepfdepf rM
MLR
The mass of U-235 in the enriched fuel annulus is:
menr,U-235 = Uenr
enrU
enrUUenrfdepfm r
M
MLRR ,,
22 )(
The mass of U-238 in the enriched fuel annulus is:
menr,U-238 = )1()( ,,
22
Uenr
enrU
enrUUenrfdepfm r
M
MLRR
where Rm is the new fuel pellet radius. Again, to calculate the thickness of the thin enriched U-metal fuel layer in Design 3, a simple mass balance relation can be formulated based on the mass of U-235 in the reference CANDU-6 and Design 3 fuel pins.
mnat,U-235 = mdep, U-235 + menr, U-235
Uenr
enrU
enrUUenrfdepfm
Udep
depU
depU
UdepfdepfUnat
OnatU
natUUnatff
rM
MLRR
rM
MLRr
MM
MLR
,,
22
,,
2
,
16
,
2
)(
*2
Based on the previous terminology for Anat,U, the above equation can be simplified to:
UenrUenrfdepfmUdepUdepfdepfUnatUnatUnatff rLRRrLRrLR ,,
22
,,
2
,,,
2 )(
The above equation can be further simplified by multiplying both sides by πLf.
UenrUenrdepfmUdepUdepdepfUnatUnatUnatf rRRrRrR ,,
22
,,
2
,,,
2 )(
UnatUnatUnatfUenrUenrmUenrUenrUdepUdepdepf rRrRrrR ,,,
2
,,
2
,,,,
2 )( (iv)
Similarly, a simple mass balance relation can be formulated based on the mass of U-238 in the reference CANDU-6 and Design 3 fuel pins.
mnat,U-238 = mdep, U-238 + menr, U-238
Page | 159
)1(*2
,
16
,
2
Unat
OnatU
natUUnatff r
MM
MLR
= )1( ,,
2
Udep
depU
depU
Udepfdepf rM
MLR
+
)1()( ,,
22
Uenr
enrU
enrUUenrfdepfm r
M
MLRR
)1()()1()1( ,,
22
,,
2
,,,
2
UenrUenrfdepfmUdepUdepfdepfUnatUnatUnatff rLRRrLRrLR
The above equation can be further simplified by multiplying both sides by πLf.
)1()()1()1( ,,
22
,,
2
,,,
2
UenrUenrdepfmUdepUdepdepfUnatUnatUnatf rRRrRrR
)1(
)1()]1()1([
,,,
2
,,
2
,,,,
2
UnatUnatUnatf
UenrUenrmUenrUenrUdepUdepdepf
rR
rRrrR
(v)
Eq. (iv) and Eq. (v) can be solved for the two unknown Rdepf and Rm by multiplying Eq. (iv) by
Uenr
Uenr
r
r
,
, )1( and subtracting it from Eq. (v). This gives:
Uenr
Uenr
UnatUnatUnatf
UenrUenrm
Uenr
Uenr
UenrUenrUdepUdepdepf
r
rrR
rRr
rrrR
,
,
,,,
2
,,
2
,
,
,,,,
2
)1(
)1()1(
)(
(vi)
Subtracting Eq. (v) from Eq. (vii) gives:
)1()1(
)]1()1([)1(
)(
,,,
2
,
,
,,,
2
,,,,
2
,
,
,,,,
2
UnatUnatUnatf
Uenr
Uenr
UnatUnatUnatf
UenrUenrUdepUdepdepf
Uenr
Uenr
UenrUenrUdepUdepdepf
rRr
rrR
rrRr
rrrR
))1()1(
(
)1()1()1()1(
,
,
,
,,,
2
,,,,,,
,
,
,,
2
Unat
Uenr
Uenr
UnatUnatUnatf
UenrUenrUdepUdepUenrUenr
Uenr
Uenr
UdepUdepdepf
rr
rrR
rrrr
rrR
Page | 160
)1()1(
)1()1(
,
,
,
,,,
2
,
,
,
,,
2
Unat
Uenr
Uenr
UnatUnatUnatf
Udep
Uenr
Uenr
UdepUdepdepf
rr
rrR
rr
rrR
)1()1(
)1()1(
,
,
,
,,
,
,
,
,,,
2
2
Udep
Uenr
Uenr
UdepUdep
Unat
Uenr
Uenr
UnatUnatUnatf
depf
rr
rr
rr
rrR
R
)1()1(
)1()1(
,
,
,
,,
,
,
,
,,,
2
Udep
Uenr
Uenr
UdepUdep
Unat
Uenr
Uenr
UnatUnatUnatf
depf
rr
rr
rr
rrR
R
Evaluating the above equation gives:
1772.07556.18
3229.3
)002.01(195.0
)195.01(002.095.18
)0071.01(195.0
)195.01(0071.08815.0*6.106075.0 2
depfR
cmRdepf 4209.0
Thickness of the depleted Uranium metal layer would be 0.4209 cm. Substituting this value back into Eq. (iv) gives:
UnatUnatUnatfUenrUenrmUenrUenrUdepUdepdepf rRrRrrR ,,,
2
,,
2
,,,,
2 )(
)( ,,,,
2
,,,
2
,,
2
UenrUenrUdepUdepdepfUnatUnatUnatfUenrUenrm rrRrRrR
UenrUenr
UenrUenrUdepUdepdepfUnatUnatUnatf
mr
rrRrRR
,,
,,,,
2
,,,
2
2)(
Page | 161
UenrUenr
UenrUenrUdepUdepdepfUnatUnatUnatf
mr
rrRrRR
,,
,,,,
2
,,,
2 )(
Evaluating the above equation gives:
195.0*95.18
)195.0*95.18002.0*95.18(*4209.00071.0*8815.0*6.10*6075.0 22 mR
18196.06953.3
)6479.0(02448.0
mR
mR 0.4266 cm
Thickness of the enriched layer then becomes:
tenrf =0.4266 cm – 0.4209 cm = 0.00567 cm