the potential effect of water influx on the …portion of the snl source-term effort consisted of...
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t 7f AND A i 1EPORIT SAND84-1007 * Unlimited Release * UC-70Printed December 1985
Nevada Nuclear Waste Storage Investigations Project
The Potential Effect of WaterInflux on the Dissolution Rateof U02 in Spent Fuel at theYucca Mounitain, Nevada Site
Jeffrey W. Braithwaite
Prepared bySandia National LaboratoriesAlbuquerque, New Mexico 87185 and Livermore, California 94550for the United States Department of Energyunder Contract DE-AC04-76DP00789
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DistributionCategory UC-70
SANDB4-1007Unlimited Release
Printed December 1985
THE POTENTIAL EFFECT OF WATER INFLUX ON THE DISSOLUTIONRATE OF U02 IN SPENT FUEL AT THE YUCCA MOUNTAIN, NEVADA SITE
by
Jeffrey W. BraithwaiteNNWSI Repository Performance Assessments Division 6312
Sandia National LaboratoriesAlbuquerque, New Mexico 87185
ABSTRACT
This study identifies the potential effect of groundwater influx on
the dissolution rate of uranium dioxide (UO2) from spent fuel for
expected conditions at a prospective site for the disposal of radioactive
waste. The analysis is based on the hydrological characteristics of the
unsaturated zone at Yucca Mountain, Nevada. Although conditions that
could lead to inundation of the waste packages are improbable at the
site, dissolution resulting from either complete or partial exposure of
the spent fuel to water was considered. Estimates were made of the lower
limit of water-contact time with the UO2 in spent fuel under partially
saturated conditions. If spent fuel is inundated, the dissolution rate
of the UO2 is constrained by its solubility limit. If partially
saturated conditions exist, the uranium dioxide leach rate could control
the dissolution process. Under conditions of both partial or complete
saturation, the dissolution rate of the uranium is shown to be a linear
function of the water influx. The practical application of the results
of this study for determining radionuclide-release rates from spent fuel
is also discussed.
i
TABLE OF CONTENTS
Page
ABSTRACT . . . . . . . . . . . . . . . . . . . . . . . . . .LIST OF FIGURES . . . . . . . . . . . . . . . . . . . . . . . . .iiiLIST OF TABLES . . . . . . . . . . . . . . . . . . . . . . . . . iv
INTRODUCTION . . . . . . . . . . . . . . . . . . . . . . . . . . 1
ASSUMPTIONS . . . . . . . . . . . . . . . . . . . . . . . . . . . 2Temperature . . . . . . . . . . . . . . . . . . . . . . . . . 2Water Chemistry .... . . . . . . . . . . . . . . . . . . . 3Water Influx . . . . . . . . . . . . . . . . . . . . . . . . 3Water Contact Time .... . . . . . . . . . . . . . . . . . 7
DETERMINATION OF THE URANIUM DIOXIDE DISSOLUTION RATE ... . . . 10Candidate Equations .... . . . . . . . . . . . . . . . . . 10Dissolution Rate as a Function of Water Flux . . . . . . . . . 14Identification of Rate-Controlling Description . . . . . . . . 19Saturated Conditions . . . . . . . . . . . . . . . . . . . . 19Partially Saturated Conditions . . . . . . . . . . . . . . . 21
APPLICABILITY TO DETERMINING RADIONUCLIDE RELEASE RATES . . . . . 21
SUMMARY . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 25
REFERENCES . . . . . . . . . . . . . . . . . . . . . . . . . . . 26
APPENDIX .... . . . . . . . . . . . . . . . . . . . . . . . . 28References . . . . . . . . . . . . . . . . . . . . . . . . . . 33
ii
LIST OF FIGURES
Firure Page
1 Pictorial representation of how water can contact thespent fuel in either a partially saturated or saturatedenvironment. 6
2 Two potential modes of water collection . . . . . . . . . 8
3 Leach rate for selected elements from spent fuel in0.03 K sodium bicarbonate at 25-C . . . . . . . . . . . . 13
4 The effect of water flux on the dissolution rate of uraniumdioxide under saturated conditions for the two potentialemplacement configurations and the applicable rate-controlling dissolution descriptions . . . . . . . . . . . 16
5 The effect of water flux on the dissolution rate of uraniumdioxide under partialiy saturated conditions for thevertical emplacement configuration and the three rate-controlling dissolution descriptions being considered . . 17
6 The effect of water flux on the dissolution rate of uraniumdioxide under partially saturated conditions for thehorizontal emplacement configuration and the three rate-controlling dissolution descriptions being considered . . . 18
7 The dissolution rate of uranium dioxide from spent fuelunder saturated conditions and for both potentialemplacement configurations . . . . . . . . . . . . . . . . 20
8 The dissolution rate of uranium dioxide from spent fuelunder partially saturated conditions and for both potentialemplacement configurations . . . . . . . . . . . . . . . . 22
lii
LIST OF TABLES
Table Pate
1 Chemical composition of the groundwater for determiningsolubility limits and leach rates . . . . . . . . . . . . 4
2 Characteristics of waste packages and of water flowthrough them. These data are given as a function ofemplacement configuration and water collection mode . . . . 9
3 Characteristics of spent fuel and spent-fuel wastepackages . . . . . . . . . . . . . . . . . . . . . . . . . 15
iv
INTRODUCTION
As part of the Office of Civilian Radioactive Waste Management
program, a feasibility study for determining the potential of Yucca
Mountain, Nevada, as a repository site for high-level radioactive waste,
is being conducted under the direction of the Nevada Nuclear Waste
Storage Investigations (NNWSI) Project of the U.S. Department of Energy
(DOE). The objective of the program is to develop facilities, processes,
and systems for safe Handling and long-term containment of radioactive
waste, in compliance with state and federal regulations, environmental
standards, and technical requirements.
The task of assessing the postclosure performance of the entire waste
isolation system at Yucca Mountain is being performed by the INWSI
Repository Assessments Division of Sandia National Laboratories (SUL).
An important part of the tools used to perform this systems assessment is
a "source term." A source term is a mathematical description of the rate
of radionuclide release as a function of time from the waste packages to
the geologic setting. A preliminary source term was developed at SNL
during the early part of 1984 that could be used in the system
performance assessments required by several NNWSI-related activities that
were ongoing during that year. These activities included the
environmental assessment, data priority studies, and eventually the site
characterization plan. A portion of the source-term development study is
detailed in this report.
Most of the pre-1984 system analyses that had been performed for
VKWSI and other projects included source terms that were based on
1) radionuclide leach rates, with release generally taken either as an
instantaneous pulse or as a linear function of time (PiSford, 1982;
de~arsily et al., 1977), or more recently 2) radionuclide solubility
limits coupled with a realistic groundwater flow rate (Thompson et al.,
1984). Other studies concerned with predicting the release rate of
radionuclides from the waste form have noted the important effect that
radionuclide solubility limits and the influx of water can have (Kerrisk,
1984; Oversby, 1983; Oztunali et al., 1983). However, none of these
studies produced results that are directly applicable to the conditions
expected within Yucca Mountain. Given this situation, the initial
-1-
portion of the SNL source-term effort consisted of analyzing the effect
of water influx on the dissolution rate of the uranium dioxide matrix of
spent fuel under conditions that could reasonably be expected at the
Yucca Mountain site. Because dissolution of the uranium matrix controls
the release of several radionuclides (Oversby and McCright, 1984;
Vandergraaf, 1980), this initial study constituted the basis for the
formulation of the principal part of the source-term model used in the
early system performance assessments, as described by Braithwaite and
Tierney (Hunter, 1984). The results of this initial portion of the
system-source-term study are given in this report. Prior to discussing
the effect of water flux on the uranium dioxide dissolution rate, the
assumed spent-fuel environment is described. In the final section, the
applicability of the U02 dissolution results to radionuclide release is
discussed.
ASSUMPTIONS
In lieu of sufficient data on hydrological, geochemical and
subsurface conditions, a number of very important assumptions were made
concerning the waste package environment. These assumptions are
concerned with the temperature of the spent fuel, the chemistry of the
groundwater, the flow of water into the emplacement borehole, and the
contact time between the spent fuel and the water. Each of these
subjects is addressed separately.
Temperature
The temperature of the spent fuel is always 250C. This is a
reasonable assumption for the following reasons:
o liquid water cannot contact the spent fuel until the spent fuel
temperature has dropped below the boiling point of the water and only
when the protective canister, as well as the Zircaloy fuel cladding,
has been breached. Recent thermal analyses indicate that spent fuel
will cool to boiling-point levels after approximately 1000 years
(Stein et al., 1984). However, studies characterizing the corrosion
-2-
behavior of proposed canister materials show a high potential for
containment times greater than 10,000 years in the Yucca Mountain
environment (Oversby and McCright, 1984). Because of this long-term
containment period, and the additional protection due to the Zircaloy
cladding (Rotbman, 1984), the waste would cool to near ambient
temperatures before contact with liquid water could be possible.
o an increase in temperature either decreases or has a minimal effect
on the solubility limit of uranium dioxide (Brush, 1979; Fullam,
1981).
o the activation energy for the leaching rate of uranium dioxide can be
either positive or negative, depending upon the composition of the
groundwater. In either case the absolute value of the activation
energy is small--approximately 20 kJ/M (Thomas, 1983; Johnson et al.,
1981).
Water Chemistry
The groundwater maintains equilibration with air at a partial
pressure of 0.2 atm oxygen. This condition produces an oxidizing
electrochemical potential in the groundwater of approximately 700 mV.
The groundwater composition used for determining the solubility limit and
applicable leach-rate calculations is as shown in Table 1. The source of
this analysis was the water sample obtained from a nearby well (denoted
J-13) located at Jackass Flats adjacent to Yucca Mountain.
Water Influx
Water flow through the unsaturated zone of Yucca Mountain should be
limited to that which corresponds to downward flux. Recent studies
(Sinnock et al., 1984; Peters et al., 1984; Braithwaite and Nimick, 1984)
of water flow through the unsaturated zone at Yucca Mountain indicate
that:
o water percolation rates are low. A flux of 0.1 mm/yr or less is
consistent with actual pressure and saturation measurements, and an
-3-
TABLI 1. Chemical composition of the groundwater used fordetermining solubility limits and leach rates.
Component Concentration (ppm)
HCO3 143
Si02 64
Na+
so4
Ca+2
18
12
No03 10
Cl- 6.4
5.5
F- 2.1
1.7
42 0.1
Fe 0.044
V 0.043
Sr 0.04
Al 0.026
Ba 0.0023
Hn 0.0011
Source: Kerrisk, 1984, based on water sample from well J-13, JackassFlats, NV.
-4-
upper bound of 1 m1/yr is probably justified. The saturated
hydraulic conductivity of the fractured host rock is probably very
high (> 1000 mm/yr).
o at these percolation rates, saturation is less than 1.0, and the
suction heads are sufficiently high that water movement will take
place only in the matrix of this highly fractured rock.
This information provides an estimate of the probable path and
quantity of water flow in and out of the emplacement horizon, but does
not assess the potential for water movement through the waste package or
through the thermally and mechanically disturbed host rock surrounding
the emplacement borehole. Because all emplacement configurations contain
an air gap between the waste package and the borehole wall, the results
given in Fernandez and Freshley (1984) can be used to predict that none
of the percolating water will actually contact the packages. This
situation leads to a probable aqueous release of near zero. However,
because release calculations must be performed to assess the performance
of the geologic setting, the following water influx/characteristics were
postulated for this study:
o both saturated (inundated) and partially saturated conditions were
considered. Because the permeability of the host rock mass is much
higher than any projected percolation rate, conditions that would
allow the waste package to become inundated would not be expected.
However, during the first several thousand years, it is conceivable
that a breech could occur in the top of a waste canister that would
allow the inside of the canister to fill with water (see Figure 1).
Another reason for including the saturated environment was to allow
the entire spent-fuel surface to be exposed to water. Because leach
rates are usually dependent on the amount of wetted surface area,
this assumption allows any surface-area effect to be bounded.
o the rate of water influx was based on the method of emplacement. Two
configurations of waste package emplacement, vertical and horizontal,
-5-
Partially Saturated Inundated
L////J//At_ \ , -_ Bz _
V d
419IA
eF
6141
Sf
661
V -- I
0i*66 6 A 4EO6 6 6
EXPOSED SPENT FUEL RODS
Figure 1. Pictorial representation of how water can contact the spent fuel ineither a partially saturated or saturated environment. The figure onthe left shows water droplets flowing over exposed U02 pellets. Thefigure on the right shows how an early breech in a waste container couldlead to inundated fuel rods.
are being considered for use at Yucca Mountain. The method of
emplacement has an important effect on the amount of water that
potentially could come in contact with each waste package for the
following reason:
the quantity of water influx was calculated assuming two
potential sources of water accumulation: 1) any percolating
water intersecting a mined area (including drifts and
emplacement boreholes) is collected and dispersed equally to all
vertically emplaced packages and 2) only the percolating water
that directly intersects the emplacement borehole contacts the
package (see Fig. 2). The first mode was used only for vertical
emplacement because horizontal boreholes will be constructed
above the-floor of all access and emplacement drifts and the
second mode is applicable to both horizontal and vertical
emplacement methods.
o all water that flows into the emplacement borehole contacts exposed
UO 2 The influence of claddings or any other waste packaging
components designed to protect the fuel and prevent exposure to water
was not considered in this study (except as previously noted to delay
the onset of dissolution until lower temperatures exist). Also, it
is expected that a substantial fraction of the water would not
contact the spent fuel because of the 60 to 70 percent void volume
that exists inside an emplacement borehole.
o a constant and uniform distribution of water flow and flux was
assumed across the entire emplacement horizon.
Water Contact Time
A relatively simple analysis was performed to determine lower limits
on the time that water can remain in contact with the UO2 surface
(contact time). A description of the analysis for the partially
saturated condition is given in the Appendix and a summary of the
important results for both partially saturated and the unexpected,
short-term saturated conditions is given in Table 2.
-7-
I I I I I I I 1%.. PERCOLATINOII I I I I I I WATER
I ~~~I I I I
m I III II I
f II
WASTE PACKAGE
MODE I
IHORIZONTAL EMPLACEMENT
VERTICAL EMPLACEMENT
MODE 2
Figure 2. Two potential modes of water collection.
NOTE: In Mode 1, all the water that would normally contact amined area (including access drifts and emplacement boreholes)is collected and evenly distributed to the waste packages.This mode is applicable only to vertical emplacement. In Mode2, only the water that contacts the emplacement borehole crosssection is available to contact the waste packages.
-8-
TABLE 2. Characteristics of waste packages and of water flow throughthem. These data are given as a function of emplacementconfiguration method and water collection mode.*
Horizontal Emplacement Vertical EmplacementFlow Hode 2 Flow Mode I Flow Mode 2
Waste package characteristics:
Borehole diameter (cm) 69 61 61Package length (cm) 450 450 450Borehole free volume (.) 70 62 62Volumetric flux 3.1 50 0.3
(liters/yr/package)
Water flow characteristics:
Inundated conditions:
Mean water retention time 380 16 2800(yr)
Partially saturated conditions (see Appendix):
Droplet flow rate 4 x 10-3 0.07 4 x 10-4(number/s/pkg)
Droplet retention time (s) 2.3 8.8 8.8
Surface area covered 1.6 x 10-7 1 x 10-5 6 x 10-8(m 2 /package)
Percentage surface area 1 x 10-7 7 x 10-6 4 x 10-8covered
C: constant in equation l 5 x 10-5 2 x 10-4 2 x 10-4(yr * m2/m3)
*NOTE: For an explanation of the two water modes, refer to the text orFig 2. All of the flow rates and area coverages shown are per mm/yr of waterflux. The water retention time for the inundated conditions was calculatedusing the information contained in the first four lines of this table.
-9-
Based on a mass balance, the surface-area coverage at any time for
partially saturated conditions is given by the following equation:
SA . C * F * A, (1)
where
SA - surface area covered (a of UO2/package)
F - flux of percolating water (m3/m2/yr)
A = effective horizontal intercept area of groundwater by the
package (m2)
C - factor accounting for the contact time of the droplets and
their ratio of contact area to volume (yr * m2 /m3)(see
Table 2 for actual values).
DETERMINATION OF THE URANIUM DIOXIDE DISSOLUTION RATE
Candidate Equations
The dissolution or leach rate of the uranium dioxide matrix
represents the kinetics of the dissolution process and is a function of
the aqueous environment and the chemical and physical properties of the
spent fuel. Leach rates are typically determined experimentally in
aqueous solution replenished often enough to ensure that any
rate-retarding effects of soluble products are not important. However,
if the leach rate is fast and little water is available, the
concentration of the solubilized product can increase to its solubility
limit. At this point, no further net dissolution will occur. Thus,
saturation of the available water with a dissolved product establishes an
upper bound on the dissolution rate.
The low level of water influx and the unsaturated conditions
expected at Yucca Mountain appear suitable to allow either solubility
limits or leach rates to control the dissolution rate. That is, if water
comes in contact with the waste for relatively long times (e.g., in a
water-filled container with breached areas only in the top), solubility
limits coupled with water influx could control the rate. On the other
hand, if the water-contact time is small (a.g., droplet flow over
-10-
individual spent-fuel rods under partially saturated conditions), leach
rates may control the dissolution. To determine which of these two
descriptions is appropriate for uranium dioxide dissolution under the
assumed conditions, the analysis detailed in the remainder of this
section was performed.
Because of the half life of uranium (4.5 x 109 years), radioactive
decay will not significantly affect the quantity of uranium available for
leaching over reasonable time periods. For convenience in this analysis,
the rate of dissolution of the uranium matrix is defined as the mass
fraction of uranium dissolved per year. This definition is related to
the curie release-rate.expression used by the NRC in 10 CFR 60 when the
total available mass is taken to be the inventory in the waste package
1000 years after closure. The mass-fraction-based release rate for the
uranium dioxide matrix is-given by equations (2) through (4) below.
For the dissolution rate controlled by the solubility limit and water
influx:
Rm =F A *.S/H , (2)
where
R = fractional release rate of the uranium dioxide matrix basedm
on mass (1/year)
Sm = solubility limit of the uranium dioxide matrix (kg/m )
im = mass of uranium contained in the waste package at the time of
closure (kg)
F = flux of percolating water (m 3/m2/yr)
A -effective horizontal intercept area of the groundwater by the
package (m2).
Equation (2) is applicable to both unsaturated and partially saturated
conditions because if all water flowing through the repository becomes
saturated, the manner in which water contacts the uranium is irrelevant.
The dissolution rate controlled by the leach rate is expressed as:
Rm = TA * SA/Mm (3)
-11-
where
LR = leach rate of the uranium matrix (kg/m /yr).
Equation (3) is directly applicable to the constantly wetted surface area
or saturated conditions under which the leach-rate measurements are made
(in this case SA - geometric surface area). Additionally, equation (1)
can be substituted into equation (3) to give an expression defining
release rate under the partially saturated conditions in which exposed
surface area may not be constant:
R = C * LB * A * F./ (4)m mn
To determine which of these two equations best describe the rate of
dissolution under the postulated conditions, site-specific information is
required concerning waste-package design, repository design, the uranium
dioxide leach rate, and the uranium dioxide solubility limit. Several
researchers have studied the dissolution characteristics of U02 in both
deionized water and carbonate-containing solutions (Wilson and Oversby,
1984; Katayama et al., 1980; Thomas, 1983; Johnson et al., 1981; Hiskey,
1979; Grandstaff, 1976). gone of these pre-1984 experimental studies
specifically used the chemical composition of the groundwater (e.g.,
150 ppm bicarbonate) or the partially saturated conditions expected at
Yucca Mountain. An initial uranium leach rate of 0.4 kg/m /yr and a
steady-state leach rate of 7 x 10 kg//m /yr were chosen from the
results shown in Fig. 3 as the most closely representative for the
expected environment. The initial leach rate is the dissolution rate
measured within the first few days after exposing fresh, unleached
uranium dioxide to a solution. The steady-state leach rate is the
dissolution rate measured after an extended exposure period (typically
greater than 1 year) by which time the rate-inhibiting effects of
alteration-product layers have become important. For more detail on the
effect of alteration products, see the last section of this report. The
initial leach rate was included in the calculations because it represents
the fastest dissolution possible in a given solution. The steady-state
-12-
ty5P'
I laTIME. days
Figure 3. Leach rate of selected elements from spent fuel in 0.03 M sodiumbicarbonate solution at 25-C.
NOTE: The leach rate given is equal to the fraction of eachelement extracted divided by the leach time interval (days) and thespecific surface area (cm2/g) of the spent fuel sample. Thisfigure was reproduced from Katayama et al. (1980).
-13-
data were included because they represent a lower bound on the dissolution
rate in solutions in which soluble products are not allowed to concentrate.
In addition, when considering release from spent fuel, Vandergraaf (1980)
concluded that leach tests must be conducted for a minimum of 300 days before
results can be regarded as meaningful. The leach-rate data given in Fig. 3
were selected because they represent the longest term data available for spent
fuel dissolution in an environment containing carbonate and because they
appear to be consistent with those identified by the other researchers. These
rates may be conservatively high (by up to a factor of 4) because, as Hiskey
(1979) noted, the uranium dioxide dissolution rate is proportional to the
square root of the carbonate concentration and Katayama's leaching solution
contained an order of magnitude higher carbonate than Yucca Mountain water
probably does.
Solubility limits for most of the important radionuclides were calculated
by Kerrisk (1984) using the geochemical code EQ3/6. For this study, only the
total solubility limit for uranium is important (0.05 kg/m ). summaries of
relevant repository layout and waste package design information are given in
Tables 2 and 3.
Dissolution Rate as a Function of Water Flux
Equations 2, 3, and 4 can be used to calculate the uranium dissolution
rate for the two rate-controlling processes being considered. As mentioned
earlier, the flux of water through the repository region has not yet been
accurately determined. Because this parameter represents the principal
unknown in both equation 2 (solubility controlled) and equation 4
(leach-rate-controlled under partially saturated conditions), the uranium
dissolution rate has been calculated and plotted in Figs. 4, 5, and 6 as a
function of water flux for the two emplacement configurations and
water-collection conditions assumed in this study. Fig. 4 represents the
response under saturated conditions for vertical and horizontal emplacement
configurations; Fig. 5 is for partially saturated conditions and vertical
emplacement, and Fig. 6 is for partially saturated conditions and horizontal
emplacement. The notation of flow mode refers to the assumption concerning
the disposition of infiltrating water that would contact a mined region (see
Fig. 2). Mode 1 yields conservatively high values for water influx, but as
explained in the assumptions section, it is
_14-
TABLE 3. Characteristics of spent fuel and spent-fuel wastepackages.
SPENT FUEL
Pin length
activetotal
Pin diameter
Pellet diameter
Cladding thickness
366 cm385 cm
0.95 cm
0.82 cm
0.057 cm
WASTE PACKAGE
Thermal power
Number/acre at57 kW/acre
Outside diameter
Length
Total weight
lumber of pins
Weight of spent-fuel components:
UraniumMetal oxideZirconiumOther hardware
Total geometric surface area of U02
3.05 kW
18.7
50 cm
450 cm
4500 kg
1584
2766314475696
149
kgkgkgkg
Source: (Bechtel, 1979; Gregg and O'Neal, 1983)
-15-
1=..
0)QasC0
CD
M._
o..'.."
0I
f-.z0
-
n0U)U)
10-5
10-6
0sI
10-8
10-9
10-10
10-11
101-2 L10-2 lo-' 100 101 102
WATER FLUX (mm/yr)
FViure 4. The effect of water flux on the dissolution rate of uranium dioxideunder saturated conditions for the two potential emplacementconfigurations and the applicable rate-controlling dissolutiondesciv.tions.
10-4
haAs
0.0Ma-
.I0
3
crz0
J0C,)U)S
10-5 :r
1 0 -6.
10-7.
10-9 ..
10-11
10-12 -
10-2
I0-j
10-1 100 10 102 103
WATER FLUX (mm/yr)
Figure 5. The effect of water flux on the dissolution rate of uranium dioxideunder partially saturated conditions for the vertical emplacementconfiguration and the three rate-controlling dissolutiondescriptions being considered.
10-4
b-
b-
W
03C0
L)
I-
V)%0
V,)
Qcc)a
10-6
10-8
10-10
10-11
Ia
10-12 L10-2 10-1 100 101 102 1o3
WATER FLUX (mm/yr)
Figure 6. The effect of water flux on the dissolution rate of uranium dioxideunder partially saturated conditions for the horizontal emplacementconfiguration and the three rate-controlling dissolutiondescriptions being considered.
applicable only to vertical emplacement because horizontal boreholes are
located above drift floors. Mode 2 represents a more realistic upper-bound
condition. Because mode 2 collection yields much lower volumes of water that
can contact the fuel, it is not surprising that solubility-based dissolution
rates, which are a linear function of water flux, are also much lower than for
mode 1 collection.
As shown in Table 2, the mean contact time of the water for saturated
conditions would be very long (16 to 2800 years). With such slow water
movement, initial leach rates that occur for the first year of exposure,
should not be important. Therefore, in Fig. 4, only steady-state leach rates
were included. On the other hand, under partially saturated conditions, both
initial and steady-state leach rates could be important. With a predicted
droplet contact time of less than 10 seconds (see Table 2), initial leach
rates would be expected to dominate until the passivating alteration product
layer had been formed. After this time, steady-state leach rates could
control the dissolution rate.
Identification of Rate-Controllinx Description
The processes that control the dissolution rate for both emplacement
methods and both water-collection modes can be identified by considering the
results shown in Figs. 4, 5, and 6. The process that produces the slowest
dissolution rate is rate controlling. That is, a solubility limit cannot be
achieved if the leach rates are too slow and, as mentioned previously, the
dissolution rate cannot cause the solibility liimit to be exceeded at any leach
rate. The justification for the controlling-process selection is given
separately for saturated and partially saturated conditions in the following
paragraphs.
Saturated Conditions. As shown in Fig. 4, dissolution based on the
solubility limit constrains the rate until unrealistically high water flux
values are reached. At this point, the steady-state leach rate, which is not
a function of the flux under these inundated conditions, begins to dominate.
Therefore, if the canister interior or emplacement borehole becomes inundated,
the uranium solubility limit should constrain the dissolution rate of the
uranium dioxide. The appropriate data are replotted in Fig. 7 in which the
effect of water flux on the controlled dissolution rate of uranium dioxide
-19-
I-
b-0)a.C0
0-IL)
nI-
'C0~
-J%0
(I)3
I
0
10-2 10-1 100 10l 102 1o 3
WATER FLUX (mm/yr)
Figure 7. The dissolution rate of uranium dioxide froa spent fuel as afunction of water flux under saturated conditions and for bothpotential emplacement configurations. The responses shown in thisfigure are based on the rate-controlling process descriptionsapplicable for these conditions. The cross-hatched area Indicatesthe currently expected range of water-flux values at the Yucca
Mountain repository horizon.
under saturated conditions is shown. The crosshatched area on this
figure indicates the water-flux range that is consistent with
hydrological calculations and field measurements at the projected horizon
for the repository at Yucca Mountain. A value of flux greater than
1 mm/yr is unlikely according to those calculations and measurements,
which are, however, consistent or lower than values of flux equal to
0.01 mm/yr. Dissolution rates at a water flux of up to 1000 mms/yr were
included in these calculations to allow the dissolution rate to be
plotted under partially saturated conditions and steady-state leach-rate
control (Fig. 5).
Partially Saturated Conditions. As shown in Figs. 5 and 6, leach
rates should control the dissolution of uranium. This results from the
very short contact times that were calculated for the partially saturated
conditions. Whereas one expects the steady-state leach rates to dominate
over the long term, the initial leach rate was selected for the remaining
calculations and discussion because of the uncertainty in droplet flow
time. The travel time for the droplet to flow over the uranium dioxide
that was used, less than 10 seconds, represents the minimum possible
value. Surface contamination, rod-to-rod contact, and the presence of
discrete joints between individual pellets could dramatically increase
droplet contact time and therefore the overall rate of dissolution.
Again, the appropriately chosen data are replotted in Fig. 8 showing the
effect of water flux on the controlled dissolution of uranium dioxide
under partially saturated conditions. The observation that a very high
leach rate can still control the dissolution rate is important because it
means leach rates must be accurately determined if realistically
appropriate source terms are to be formulated.
APPLICABILITY TO DETERMINING RADIONUCLIDE RELEASE RATES
The dissolution rate of the uranium dioxide matrix of spent fuel-
plays an important role in determining the release rate of a number of
fission product and actinide radionuclides that are physically separated
from a leaching groundwater by this relatively impermeable matrix. For
-21-
he.
:0
A-
a.Cn0-
s
co
-
O)0)
cc
0
J0CoU)
nQo
I3
IJ
10-2 lo-' 100 lo 102 103
WATER FLUX (mm/vr)
vigure B. The dissolution rate of uranium dioxide from spent fuel as afunction of water flux under partially saturated conditions and forboth potential emplacement configurations. The responses shown inthis figure are based on the rate-controlling process descriptionsapplicable for these conditions. The cross-hatched area indicatesthe currently expected range of water-flux values at the YuccaMountain Repository horizon.
several radionuclides that are not contained within the matrix (e.g.,
portions of cesium, technetium, carbon, and iodine), the dissolution of
the matrix is unimportant.
In this subsection, information is presented to show why a modified
congruent-alteration mechanism is currently a reasonable approach that
would allow the release rate for the appropriate radionuclides to be
determined. In this discussion, congruent alteration simply means that
the availability or exposure of radionuclides to the aqueous environment
is limited by the extent of aqueous alteration of the uranium dioxide
matrix. As a portion of the matrix reacts with the groundwater, all
species contained within that portion are also subject to contact with
the groundwater. In addition, it can be assumed that once the matrix is
altered, all available species within that element, including uranium,
are solubilized. Thus, no solid layer of alteration products forms and,
with a uniform distribution of radionuclides throughout the spent fuel,
the fractional rate of dissolution of the other species is restricted to
the fractional rate of alteration of the uranium matrix. This mechanism
has been termed "congruent alteration" to distinguish it from the more
frequently discussed "congruent leaching" mechanism. Whereas most
characterization studies of spent-fuel dissolution support the conclusion
that species contained in the unleashed portions of the matrix undergo
congruent alteration with the matrix, there exists considerable confusion
as to whether these same species are actually solubilized in a congruent
manner (congruent leaching). Congruent alteration with complete product
solubilization is a conservative form of congruent leaching, and the
assumption that it controls the release of several radionuclides is
currently justified for the following reasons:
a) The presence of a rind layer consisting of solid reaction products
on the surface of dissolving spent fuel (Thomas, 1983) can play an
important role by forcing experimentally measured (or apparent)
individual release rates to deviate from those predicted simply by
matrix dissolution. This deviation occurs primarily for two
reasons: 1) A precipitation effect: Primarily because reactants
diffuse inward and soluble products diffuse outward through this
rind layer, the aqueous chemistry at the reacting interface is
different from the chemistry in the external groundwater.-23-
This chemical difference allows solid hydrated oxy-uranium products
of varying composition to precipitate as this rind layer. This
precipitation process selectively removes solubilized radionuclides,
and 2) A passivation effect: Oxygen has been shown to be a key
reactant in natural groundwaters because the leach rate of uranium
dioxide is dependent on the dissolved oxygen concentration (Hiskey,
1979; Grandstaff, 1976; Johnson, 1981). Therefore, for the
continued dissolution of uranium to occur, oxygen must diffuse
through the rind layer to the unreacted core interface. This
diffusion process causes the oxygen concentration at the interface
to be lower than in the bulk solution. The passivating effect (#2)
and the variable precipitation effect (#1) could account for a major
portion of both the decrease and the spread observed experimentally
in spent-fuel leach rates (see Fig. 3). By assuming congruent
alteration with soluble products, the inhibiting effects of oxygen
diffusion and solid-product formation are ignored and all species
are solubilized at the maximum rate possible.
b) Some oxidation of the uranium dioxide matrix, along with segregation
of many nonuranium species, occurs during irradiation and
preparation of experimental samples (Katayama et.al, 1980;
Vandergraaf, 1980). These processes, in conjunction with a newly
forming alteration layer, require that care be exercised when
applying short-term experimental dissolution data to the formulation
of conclusions concerning congruent alteration. To illustrate this
point, only 0.075% of a typical -2 + 4 mm fuel fragment (i.e., a
fragment with an equivalent spherical diameter between 2 and 4 mm)
would dissolve each year into large excesses of deionized water.
This rate corresponds to only 1 um/yr of penetration. With such
slow reaction rates, short-term data generally reflect the leaching
characteristics of the exposed, potentially perturbed surface and
not any bulk material.
-24-
c) If the composition and thickness of the alteration product layer
reaches steady-state values, then individual radionuclide release
rates should follow a congruent-leaching mechanism. A Canadian
researcher (Thomas, 1983) concluded that this is indeed the case in
the long term. Furthermore, the spent-fuel leach data shown in
Fig. 3 for periods greater than 1 year, generally shows a trend
toward congruent leaching. Finally, the conclusion was reached in a
review conducted for the VRC that the actinide products dissolve
congruently (Dayal et al., 1982). The actinides may be the primary
concern with an expected containment time of 1,000 to 10,000 years.
-SUMMARY
The effect of water flux or percolation rate on the dissolution of
uranium dioxide from spent fuel was investigated for conditions that
could be encountered within a waste package emplaced at Yucca Mountain.
Despite the low probability that spent fuel would be exposed to water,
allowances were made in this study for the occurrence of a breech in the
waste container and for partial or complete saturation. The most
significant results of this study indicate that:
1. If the spent fuel is saturated, the dissolution rate of the uranium
dioxide will be constrained by its solubility limit and the influx
of water.
2. If the spent fuel is exposed only to partially saturated conditions,
as is currently expected, then the leach rate of the uranium dioxide
should control its rate of dissolution.
3. The release rate of many nonuranium radionuclides can reliably be
predicted, using a congruent matrix alteration mechanism with
complete product solubilization.
-25-
REFERENCES
Bechtel National, Inc., "An Assessment of LWR Spent Fuel DisposalOptions," ONWI-39, Battelle Memorial Institute, Vol 3, July 1979, p.A-14.
Braithwaite, J. W., and F. B. Nimick, "Effect of Host-Rock Dissolution andPrecipitation on Permeability in a Nuclear Waste Repository in Tuff,"SAND84-0192, Sandia National Laboratories, September 1984, p. 35-39.
Brush, L. H, "The Solubility of Some Phases in the SystemU03-Na2 O-H20 in Aqueous Solutions at 60 and 900C," Ph.D.Dissertation, Harvard University, June 1980, p. 155.
deHarsily, G., et al., "Nuclear Waste Disposal: Can the GeologistGuarantee Isolation?," Science, 197 (4303), August 5, 1977, p. 520.
Dayal, R., at al., Nuclear Waste Management Technical Support in theDevelopment of Nuclear Waste Form Criteria for the NRC,"NUREG/CR-2333, U.S. Nuclear Regulatory Commission, February 1982,p. 18-39.
Fernandez, J. A., and H. D. Freshley, "Repository Sealing Concepts forthe Nevada Nuclear Waste Storage Investigations Project,"SAND83-1778, Sandia National Laboratories, August 1984, p. 33.
Fullam, H. T., "Solubility Effects in Waste-Glass/Demineralized-WaterSystems," PNL-3614, Pacific Northwest Laboratories, June 1981,p. 30-32.
Grandstaff, D. E., "A Kinetic Study of the Dissolution of Uraninits,"Econ. Geol., 71 (8), 1976, pp. 1495-1497, 1500.
Gregg, D., and W. O'Neal, "Initial Specifications for Nuclear WastePackage External Dimensions and materials," UCID-19926, LawrenceLivermore National Laboratories, September 1983.
Hiskey, J. B., "Kinetics of Uranium Dioxide Dissolution in AmmoniumCarbonate," Trans C Inst Min Metal, 88, 1979, p. 146-148.
Hunter, T. 0., and A. B. Muller, "Proceedings of the Workshop on theSource Term for Radionuclide Migration for High-Level Waste or SpentNuclear Fuel Under Realistic Repository Conditions," SAND85-0380,Sandia National Laboratories, July 1985, pp. 71-75.
Johnson, L. H., et al., "The Dissolution of Unirradiated Uranium DioxideFuel Under Hydrothermal Oxidizing Conditions," AECL-TR128, AtomicEnergy of Canada, LTD. April 1981, pp. 1, 2, 8, 10.
Katayama, Y. B., et al.,"Status Report on LWR Spent Fuel IAEA LeachTests," PNL-3173, Pacific Northwest Laboratories, March 1980, pp.3-9, 28.
-26-
Kerrisk, J. F., "Solubility Limits on Radionuclide Dissolution at a YuccaMountain Repository," LA-9995-MS, Log Alamos National Laboratory, May1984, pp. 1, 5, 32.
Oversby, V. M., "Performance Testing of Waste Forms in a TuffEnvironment," UCRL-90045, Lawrence Livermore National Laboratory,November 1983, p. 10.
Oversby, V. M., and R. D. McCright, "Laboratory Experiments Designed toProvide Limits on the Radionuclide Source Term for the NNWSIProject," UCRL-91257, Lawrence Livermore National Laboratory,November 1984, p. 6.
Oztunali, 0. I., et al., "Influence of Leach Rate and Other Parameters onGroundwater Migration," NUREG/CR-3130, Nuclear Regulatory Conmiission,February 1983.
Peters, R. R., et al., "Fracture and Matrix Hydrologic Characteristics ofTuffaceous Materials from Yucca Mountain, Nye County, Nevada,"SAND84-1471, Sandia National Laboratories, December 1984, p. 58-60.
Pigford, T. H., "Geological Disposal of Radioactive Waste," ChemicalEngineering Progress (CEP), pp. 18-26, March 1982, p. 18-19.
Rothman, A. J., "Potential Corrosion and Degradation Mechanisms ofZircaloy Cladding on Spent Nuclear Fuel in a Tuff Repository," UCID20172, Lawrence Livermore National Laboratory, September 1984, p. 40.
Sinnock, S., et al., "Preliminary Bounds on the Expected PreclosurePerformance of the Yucca Mountain Repository Site, Southern Nevada,"SAND84-1492, Sandia National Laboratories, December 1984, p. 13-14.
Stein, W., et al., "Thermal Analysis of NNWSI Conceptual Waste PackageDesigns," UCID-20091, Lawrence Livermore National Laboratory, April1984, p. 66-70.
Thomas, G. F., "The Dissolution of Unirradiated Uranium Dioxide FuelPellets," AECL-TR234, Atomic Energy of Canada, LTD, November 1983,pp. 2, 3, 7, 10-13.
Thompson, F. L., F. H. Dove, and K. M. Krupka, "Preliminary Upper-BoundConsequence Analysis for a Waste Repository at Yucca Mountain,Nevada," SAND 83-7475, Sandia National Laboratories, August 1984,p. 13.
Vandergraaf, T. T., "Leaching of Irradiated Uranium Dioxide Fuel,"AECL-TR100, Atomic Energy of Canada, LTD, May 1980, p. 13.
Wilson, C. N., and V. M. Overgby, "Spent-Fuel Cladding Containment CreditTests," UCRL 89869, Lawrence Livermore National Laboratory, September1984, p. 6-8.
-27-
APPENDIX
CHARACTERISTICS OF WATER FLOW OVER URANIUM DIOXIDE IN SPENT FUEL
IN AN UNSATURATED ENVIRONMENT
The analysis that was performed to determine the flow characteristics
of water over spent-fuel rods in an unsaturated environment is detailed
in this section. This initial study, although relatively simple in
scope, was performed so that any leach-rate affects on the dissolution of
spent fuel could be included in this report. The author is grateful to
Tom Hinkebein of Division 6257 of Sandia National Laboratories for his
valuable discussions concerning this analysis.
The primary assumption used in this analysis is that all water that
enters the emplacement borehole contacts bare spent fuel. As such, the
protective metal barriers (the container and Zircaloy cladding) have
corroded away, exposing the spent fuel with sufficient cladding remaining
only to support the spent-fuel pellets in an intact rod configuration.
With the very low water percolation rates expected through the
repository horizon (less than 50 1/yr/package) and the high geometric
surface areas per package (150 m 2), water would be expected to flow
over the spent fuel either in very thin films or possibly
intermittently. Levich (1962) points out that if a liquid film becomes
thin enough, the action of capillary forces will cause it to break up
into droplets. The velocity of a thin film flowing down a vertical
surface can be calculated using the following equation (Levich, 1962;
Szekely and Themelis, 1971):
K2V =LI (1)3',
where
V = velocity of the film over its horizontal cross section
h . film thickness
v = kinematic viscosity of water.
-28-
Performing a mass balance for a horizontal emplacement configuration,
complete wetting, and a percolation rate of 1 mm/yr, the steady-state
average velocity of the film must equal
1.21 x 10 cm/sec (2)
Equating equations 1 and 2 and solving for h results in an average film
thickness, under these given conditions, of only 5 micrometers. Since
this thickness is several orders of magnitude less-than the equivalent
hydrodynamic boundary layer thickness (the thickness at which the liquid
gains 10% of the bulk fluid velocity) for similar flow conditions around
rotating disks (Sohn and Wadsworth, 1979), it is unreasonable to expect
the film to move as a sheet. Thus, the flow should occur in discrete
droplets.
In order to identify both the size and the velocity of droplets
flowing down the surface of a spent-fuel rod, it is assumed that the
droplets remain approximately hemispherical and that a difference exists
between the advancing and receding contact angles in the droplets.
Adamson (1960) notes that this difference in contact angle has been
observed for water flow on many mineral surfaces. Based on data
contained in the Adamson reference, an advancing angle of 65 degrees and
a receding angle of 30 degrees *ere used.
For an approximately hemispherically shaped droplet flowing down a
vertical surface, the dynamic force balance is expressed as
Au dV =--r2i dV + vry(cose - cosO ) + mg (3)dt dy a r
-29-
where
m = droplet mass
V = droplet velocity
r = droplet radius
t = time
U = viscosity of the water
y = distance perpendicular to the surface
y = surface tension of the water
ea ' advancing contact angle and
Or = receding contact angle
The four terms in equation (3) account for the total force on the
droplet, viscous drag, surface-tension effects, and weight, respectively.
In order to calculate the maximum stationary droplet size, the
acceleration (or total force), and viscous drag terms can be set to zero
because under these conditions V = 0, and the resultant equation is
solved for r.
ir Y(cose -cosO ) +-2wr3 p 0 (4)crit a r 3 crit PS
1
3(cosO - Cosa) (2[3tC°Sr °Sa) 0.221 cm (5)
rcrit l 2pg
where rcrit = maximum stationary droplet radius (surface tension forces
balance weight), and p = liquid density.3
This critical size results in a droplet volume of 0.023 cm , and a
weight of 0.023 g. This size appears reasonable because a medicine
dropper typically produces droplets with a volume of 0.05 cm3.
-30-
If it is now assumed that a droplet that is 1% larger than the
critical size calculated above will flow down the rod, then the dynamic
force balance (Equation 3) can be solved for the flow velocity as a
function of position. First, a linear velocity gradient existing across
the droplet can be assumed by realizing the maximum velocity (Vm)
occurs at the outer edge of the droplet. Therefore,
dY Vmaxdy - r (6)
Use of this assumption effectively forces the entire droplet to travel
with velocity, Vmax. Integrating Equation 6 into Equation 3 results in:
2 2 dV 2 23r dt ~Y(eos6a- coser) 3 gp mz (7)
or
V
dt 1 2 m
where
3y(cosea - coser)C a - &2 +
2r2p
and
2 a2r p
(8)
-31-
The solution to this linear ordinary differential equation with the
initial condition that at t = 0, V = 0, has the form:
CI -C t-C (1-e ). (9)C2
Since V = dx/dt, integration of equation (9) yields the solution to
the distance traveled as a function of time
CI CI -C~tx 1 t + e 2 + K (10)
C2 C22
At t - 0, x 0 and
-Cl
C 22
For the conditions expected at Yucca Mountain,
C a 19.328 cmu/s 21C2 = 0.3012 /s
K = -213.05 cm.
Therefore,
x = 64.17t + 213.05e-0 .301 2 - 213.05 (11)
where x is in cm and t in seconds.
For vertical emplacement, the maximum height of uranium dioxide pellets
is 366 cm.
-32-
In order to apply these results to a horizontally emplaced spent-fuel
package and still maintain the actual geometric surface area of the rods,
the spent fuel was assumed to be a collection of 48 individual
0.82-cm-thick flat plates with a height of 42.5 cm. This height is
equivalent to the mean segment length (1.7R) of a circular cross section
with a diameter of 50 cm. Therefore, for horizontal emplacement, the
maximum height of the uranium dioxide is 42.5 cm.
The droplet retention times shown in the text in Table 2 were
iteratively calculated using these maximum distances and equation (11).
It is important to note that the surface coverages, which are based
on the contact times and-droplet-size, are very small. This result
implies that the inflowing water does not have to be uniformly
distributed across all spent fuel rods in each package and that the
spent-fuel pellets do not all have to be exposed.
References
Adamson, A. W., Physical Chemistry of Surfaces, Interscience Publishers,New York, NY, 1960, pp. 359-362.
Levich, V. G., Physiochemical Hydrodynamics, Prentice-Hall, Inc.,
Englewood Cliffs, NJ, 1962, pp. 669-672.
Sohn, H. Y., and M. E. Wadsworth, Rate Processes of Extractive Hetallurgy,Plenum Press, New York, NY, 1979, pp. 210-220.
Szekely, J., and M. J. Themelis, Rate Phenomena in Process Metallurgy,Wiley-Interscience, Mew York, fiY, 1971, pp. 57-62.
-33-
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