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Transcript of Variable-density groundwater flow and solute transport in porous media containing nonuniform...
Advances in Water Resources 28 (2005) 1351–1367
www.elsevier.com/locate/advwatres
Variable-density groundwater flow and solute transport inporous media containing nonuniform discrete fractures
Thomas Graf *, Rene Therrien
Departement de Geologie et Genie Geologique, Universite Laval, Ste-Foy, Quebec, Canada G1K 7P4
Received 10 September 2004; received in revised form 15 April 2005; accepted 15 April 2005
Available online 20 June 2005
Abstract
Variations in fluid density can greatly affect fluid flow and solute transport in the subsurface. Heterogeneities such as fractures
play a major role for the migration of variable-density fluids. Earlier modeling studies of density effects in fractured media were
restricted to orthogonal fracture networks, consisting of only vertical and horizontal fractures. The present study addresses the phe-
nomenon of 3D variable-density flow and transport in fractured porous media, where fractures of an arbitrary incline can occur. A
general formulation of the body force vector is derived, which accounts for variable-density flow and transport in fractures of any
orientation. Simulation results are presented that show the verification of the new model formulation, for the porous matrix and for
inclined fractures. Simulations of variable-density flow and solute transport are then conducted for a single fracture, embedded in a
porous matrix. The simulations show that density-driven flow in the fracture causes convective flow within the porous matrix and
that the high-permeability fracture acts as a barrier for convection. Other simulations were run to investigate the influence of frac-
ture incline on plume migration. Finally, tabular data of the tracer breakthrough curve in the inclined fracture is given to facilitate
the verification of other codes.
� 2005 Elsevier Ltd. All rights reserved.
Keywords: Numerical modeling; Fractured rock; Inclined fracture; Contaminant transport; Density; Instability; Buoyancy term
1. Introduction
In subsurface environments, contaminants are mainly
transported by groundwater. The transport pattern isgreatly affected by the physical parameters of both the
medium and the contaminant. The transport properties
of the fluid, such as viscosity and fluid density, can also
have a significant impact on contaminant transport. The
fluid density q (fluid mass per unit volume of fluid) can
not always be assumed uniform. It decreases with
increasing temperature, increases with increasing salinity
and increases with increasing pressure due to fluidcompressibility.
0309-1708/$ - see front matter � 2005 Elsevier Ltd. All rights reserved.
doi:10.1016/j.advwatres.2005.04.011
* Corresponding author.
E-mail address: [email protected] (T. Graf).
Spatial variations of fluid density play an important
role in contaminant migration within various geological
media. If, for example, a fluid of high density overlies a
less dense fluid, the system is potentially unstable anddensity-driven flow may take place, which levels out
the density stratification and eventually stabilizes the
system. Additionally, if flow is transient, there are tem-
poral changes in density. Examples for density-driven
flow and transport can be found in many areas of sub-
surface hydrology, oceanography, meteorology, geo-
physics and hazardous waste disposal.
The safe disposal of hazardous chemicals is com-monly regarded as feasible in low-permeability geologi-
cal media at a depth of up to 1000 m [4]. In Canada, one
conceivable host rock for the repository of radioactive
waste is the crystalline metamorphic rock of the Cana-
dian Shield. Here, the groundwater at depths greater
Nomenclature
• scalar variables are denoted in normal italic
letters• vector variables are denoted in bold small
letters
• matrix variables are denoted in bold capital
letters
Latin letters
2b fracture aperture [L]
c solute concentration, expressed as relativeconcentration [–]
Dd free-solution diffusion coefficient [L2 T�1]
Dij coefficients of hydrodynamic dispersion ten-
sor [L2 T�1]
Dfrij hydrodynamic dispersion coefficient of the
fracture [L2 T�1]
f three-dimensional function, defined over a
surface S; f = f(x,y,z) [–]f global boundary flux vector [L2 T�1]
F function that defines the surface S in three
dimensions; F(x,y,z) = constant [–]
g acceleration due to gravity [L T�2]
g global body force vector [L2 T�1]
h0 equivalent freshwater head [L]
H hypotenuse of a rectangle [L]
H global conductance matrix [L T�1]i unit vector in x-direction [–]
I+, I� fracture–matrix interface [–]
j unit vector in y-direction [–]
J Jacobian matrix [–]
k unit vector in z-direction [–]
K0ij coefficients of hydraulic conductivity tensor
of freshwater [L T�1]
K fr0 hydraulic freshwater conductivity of the frac-
ture [L T�1]
‘v geometry of the model domain; v = x, y, z [L]
Lv geometry of a block element; v = x, y, z [L]
LTG characteristic length scale [L]
Nfe total number of fracture elements in the do-
main [–]
p vector that is normal to region R [–]
P dynamic pressure of the fluid [M L�1 T�2]Peg grid Peclet number [–]
qi Darcy flux [L T�1]
R vertical projection of S on a coordinate plane
[–]
Re Reynolds number [–]
s axis along a sloped tube [L]
S fluid mass matrix [L]
S surface, defined by the function F(x,y,z) =
constant [L2]SS specific storage [L�1]
Sop specific pressure storativity [M�1 L T2]
t time [T]
vi linear flow velocity [L T�1]
wi approximation function [–]
Greek letters
afl coefficient of the compressibility of the fluiddue to fluid pressure or hydraulic head varia-
tions [M�1 L T2]
afr fracture dispersivity [L]
al matrix longitudinal dispersivity [L]
am coefficient of the compressibility of the por-
ous medium due to fluid pressure or hydrau-
lic head variations [M�1 L T2]
at matrix transverse dispersivity [L]b ratio of saltwater density to freshwater den-
sity [–]
c maximum relative density [–]
dij Kronecker delta function [–]
gj indicator for the fracture face orientation [–]
j intrinsic permeability in a sloped tube [L2]
jij coefficients of the intrinsic permeability ten-
sor [L2]l dynamic viscosity of the fluid [M L�1 T�1]
m kinematic viscosity of the fluid [L2 T�1]
q fluid density [M L�3]
q0 reference fluid density [M L�3]
qr relative fluid density [–]
s factor of tortuosity [–]
u fracture incline [1�]/ porosity of the rock matrix [–]v global coordinates; v = x, y, z [L]�v local coordinates; �v ¼ �x; �y;�z [L]
Special symbols
o partial differential operator [–]
$ Nabla or divergence operator; rð Þ ¼ oð Þox þ
oð Þoy þ oð Þ
oz [L�1]
Sub- and superscripts
0 freshwater [–]
fe fracture element [–]
fr fracture [–]
i, j spatial or nodal indices [–]
n normal direction [–]
1352 T. Graf, R. Therrien / Advances in Water Resources 28 (2005) 1351–1367
than 800 m is a Ca–Na–Cl brine with dissolved solids
exceeding 100,000 mg l�1 [8]. Therefore, the density of
such deep fluids varies dramatically with solute concen-
tration. Acute safety questions regarding nuclear waste
T. Graf, R. Therrien / Advances in Water Resources 28 (2005) 1351–1367 1353
repository arise due to the presence of fractures in the
hard rock formations of the Canadian Shield. Fractures
have a great impact on the mass transport, because they
represent preferential pathways where accidentally re-
leased radionuclides might migrate at velocities that
are several orders of magnitude larger than within therock matrix itself. Clearly, it is of paramount impor-
tance to understand the movement of contaminants in
fractured media under the influence of fluctuating water
density.
In the last century, the foundations for modeling den-
sity-driven flow and transport were laid by Rayleigh
[20]. He mathematically formulated the principles that
govern the onset of instabilities caused by thermally in-duced fluid density variations in porous media. Vari-
able-density flow has been investigated experimentally
and numerically for half a century, beginning with the
experimental studies by Elder [6] and Taylor [29].
Improvements in computer performance have enabled
increasingly precise and complex simulations of density
effects, predominantly in porous media (Fig. 1a and b).
In homogeneous porous media, variable-density flowand transport have recently been studied in experimental
and numerical simulations in the fields of (i) convection
beneath salt lakes [25,26,35], (ii) seawater intrusion in
coastal aquifers [12,36], (iii) infiltration of leachates
Fig. 1. Different styles of geological media: (a) homogeneous porous medium
vertical and horizontal fractures and (d) fractured geological medium with no
In (a) and (b), the shades of grey represent hydraulic conductivity.
from waste disposal sites [9] and (iv) the analysis of
instability development [15,22,34].
In heterogeneous porous media, Schincariol and Sch-
wartz [21] were the pioneers in experimentally investigat-
ing density dependent flow and transport in layered and
lenticular media. They found that (i) the transport pat-tern in the layers is greatly sensitive to hydraulic conduc-
tivity and (ii) the heterogeneities in the lenticular
medium create relatively large dispersion that tends to
dissipate instabilities. Thus, Simmons et al. [27] infer
that heterogeneities play opposite roles in the generation
and growth of instabilities. On one hand, they are the
trigger mechanism for the onset of instabilities while
on the other hand, heterogeneities play the most impor-tant role in diminishing instabilities, once they are gen-
erated. Simmons et al. [27] showed that the style of
heterogeneity in a porous medium will greatly influence
the propagation of dense plumes, with disorganized het-
erogeneity tending to dissipate convection by mixing
and thus reducing plume instabilities. Prasad and Sim-
mons [18] confirmed this observation. They carried out
numerical variable-density transport simulations in aheterogeneous porous media. Prasad and Simmons
[18] used a modified form of the Elder [7] problem,
where the permeability was randomly distributed to
study the effects of heterogeneity on solute transport
, (b) heterogeneous porous medium, (c) fractured medium consisting of
nuniform fracture aperture, trace and orientation (modified from [27]).
1354 T. Graf, R. Therrien / Advances in Water Resources 28 (2005) 1351–1367
processes. Diersch and Kolditz [5] and Holzbecher [11]
provide an excellent overview of prior modeling work
in porous media, clearly showing that there is currently
a lack of models that take into account the crucial influ-
ence of fractures.
As opposed to the study of variable-density flow inporous media, laboratory experiments in fractured med-
ia have not yet been carried out. A ground-breaking
study in this field was published by Shikaze et al. [24]
who numerically simulated variable-density flow and
transport in discretely fractured media. They found that
vertical fractures of aperture as small as 50 lm signifi-
cantly increase contaminant migration relative to the
case where fractures are absent. Interestingly, it was alsoshown that dense solute plumes may develop in a highly
irregular fashion and are extremely difficult to predict.
However, Shikaze et al. [24] limited their studies to a
regular fracture network consisting of only vertical
and horizontal fractures, embedded in a porous matrix
(Fig. 1c). Therefore, the development of dense plume
instabilities in a discrete fracture of an arbitrary incline
remains unknown. Moreover, a network of fractureshaving irregular orientations will exhibit a different style
of heterogeneity, as opposed to regular fracture distribu-
tion, which may affect dense plume migration as sug-
gested by Simmons et al. [27].
The goal of this study is to investigate variable-den-
sity flow and transport in discretely fractured porous
media where the fracture network is lacking a regular
pattern and where fractures of an arbitrary slope can oc-cur (Fig. 1d). An existing model that solves 3D flow and
transport in discretely fractured porous media has been
modified to simulate density-dependent flow and trans-
port and to discretize discrete 2D fractures of any orien-
tation. Unlike previous studies [24], this work is not
limited to flow in orthogonal fracture networks but fo-
cuses on the growth of instabilities in an inclined frac-
ture, located in a low-permeability porous matrix.Thus, the present investigation will enable the numerical
simulation of variable-density transport in complex,
irregular fracture networks, which more closely resemble
nature.
2. Mathematical modeling
2.1. The FRAC3DVS model
FRAC3DVS is a saturated–unsaturated numerical
groundwater flow and solute transport model [30,31].
The governing equations for flow and transport are de-
rived from the continuum approach. A control volume
finite element method is used to spatially discretize the
flow and transport equations. The porous, low-perme-ability matrix is represented by regular three-dimen-
sional blocks and fractures of high permeability are
represented by two-dimensional rectangular planes.
Using undistorted finite elements allows an analytical
discretization of the governing equations by means of
elemental influence coefficient matrices [9,30]. Thus,
there is no need to numerically integrate. The solution
takes into account advective flow and transport, molec-ular diffusion, and mechanical dispersion in both the
fractures and the matrix.
In FRAC3DVS, vertical and horizontal fractures are
incorporated into the grid by superimposing two-dimen-
sional face elements onto the three-dimensional grid,
consisting of regular block elements. Two-dimensional
faces represent the fracture whereas three-dimensional
blocks denote the porous matrix. In order to fully cou-ple the fracture with the porous matrix, faces and blocks
share common nodes along the fracture walls. Thus,
nodes at fracture locations receive contributions from
both the block elements as well as from the fracture
faces. Furthermore, for these mutual nodes, both
hydraulic head and concentration at the fracture/matrix
interface are assumed to be equal. Therefore, it is not
necessary to explicitly calculate the exchange terms qnand Xn in Eqs. (14) and (16), respectively. This discrete
fracture approach has previously been applied by several
authors [28,23,30,24] and its description is, therefore,
not repeated here.
2.2. Model development
The model FRAC3DVS has been modified here toincorporate inclined fractures in the simulation of vari-
able-density flow and transport. Density variations
cause weak nonlinearities in the flow equation. In the
numerical model they are treated by means of a sequen-
tial iterative approach (SIA), also called Picard itera-
tion, which links the two governing equations for flow
and transport. This method alternately solves the two
governing equations during each time step until conver-gence is attained.
2.2.1. Discretizing inclined fractures
Similar to the integration of horizontal and vertical
(i.e. regular) fractures, inclined fractures are incorpo-
rated in the finite element grid by superimposing two-
dimensional fracture faces onto the block elements of
the porous matrix. While the six faces on the outer sur-face of the block elements can be used for the discretiza-
tion of regular fractures, for inclined fractures an
additional six inclined faces inside the blocks are also
available. Fig. 2 exhibits the orientation of the six in-
clined faces. Note that the two faces in the block on
the right of Fig. 2 are not inclined but vertical. However,
for convenience, they are considered as inclined as well
because they do not correspond to a boundary face ofthe block. Furthermore, it can be seen that all available
six element boundary faces and six inclined faces are
Fig. 2. Inclined faces in three-dimensional block elements.
T. Graf, R. Therrien / Advances in Water Resources 28 (2005) 1351–1367 1355
rectangular and undistorted. Using the control volume
finite element method, and assuming continuity of
hydraulic head and concentration at the common frac-
ture–matrix nodes, results in an unchanged connectivity
pattern for the 3D porous medium elements, irrespective
of the presence of fractures.
In FRAC3DVS, the location of three-dimensional in-
clined fractures is defined by two points and by a coor-dinate axis parallel to the fracture. The fracture shown
in Fig. 3 is parallel to the y-axis and defined by the
two points West (W) and East (E) that coincide with
the beginning and the end of a fracture. The fracture
nodes betweenW and E are selected using a simple least
distance criterion: for every node P that defines the frac-
ture, the distance of all three neighbor nodes of P to the
undiscretized fracture is calculated. The neighbor nodewhose distance to the fracture is the smallest is selected
as a fracture node and becomes point P for the next
step. Initially, P is identical to W. This process is re-
peated until the point P meets the end point E. Fig. 3
is an example of how an inclined fracture is discretized
in an irregular, relatively coarse grid. Note that the grid
is 3D with a unit thickness. Thus, the fracture is 2D and
defined by W and E and by its orientation (parallel tothe y-axis).
Inclined fractures are a combination of inclined, hor-
izontal and vertical faces. The mathematical formula-
tion of density effects in each of these three types of
fracture elements is described in the following section.
W
E
x
z
P 3
21
fracture in nature
discretized fracture
Fig. 3. Selecting two-dimensional elements of an inclined fracture.
2.2.2. Constitutive equations
The model uses the equivalent freshwater head h0 [L],
defined by Frind [9] as
h0 ¼P
q0gþ z ð1Þ
where P [M L�1 T�2] is the dynamic fluid pressure, q0
[M L�3] is the reference fluid density, g [L T�2] is the
gravitational acceleration and z [L] is the elevation above
datum. The transport variable is the dimensionless rela-
tive concentration, c, which varies between 0 and 1. It islinked with density through the linear relationship
qr ¼ cc ð2Þwhere qr is the dimensionless relative density, defined by
Frind [9] as
qr ¼qq0
� 1 ð3Þ
where q [M L�3] is the fluid density. The dimensionless
constant c is the maximum relative density given by
c ¼ qmax
q0
� 1 ð4Þ
where the assumption is made that the solute concentra-
tion of a fluid with the density q = qmax is cmax = 1. It is
also assumed that the impact of salinity on fluid viscos-
ity is negligible.Under variable-density flow conditions, the Darcy
flux, qi = /vi [L T�1], is a function of both the physical
flow variable, h0, and the chemical property, qr. The
Darcy flux in porous media can be completely expressed
in terms of freshwater properties [9]:
qi ¼ �K0ij
oh0oxj
þ qrgj
� �i; j ¼ 1; 2; 3 ð5Þ
where the assumption of a horizontal datum (i.e. oz/
oz = 1) is made and where gj [–] represents the directionof flow with gj = 0 in the horizontal directions and gj = 1in the vertical direction [9]. Assuming that fluid viscosity
does not depend on salt concentration allows the use of
the freshwater hydraulic conductivity of the porous
medium, K0ij [L T�1], given by [1] as:
K0ij ¼
jijq0gl0
ð6Þ
1356 T. Graf, R. Therrien / Advances in Water Resources 28 (2005) 1351–1367
where jij [L2] is the matrix permeability and where l0 [M
L�1 T�1] is the reference fluid viscosity. A three-dimen-
sional Cartesian coordinate system is assumed, where
the axes are co-linear with the principal directions of
anisotropy. With this assumption, cross terms (K0ij where
i5 j) in the hydraulic conductivity tensor vanish.The Darcy flux in differently oriented two-dimen-
sional fracture faces can be calculated using the follow-
ing form of the Darcy equation, presented by Bear [1]
for an inclined one-dimensional tube
qs ¼ � jl
oPos
þ qgozos
� �ð7Þ
where s [L] is the axis along the tube and where j [L2] is
the permeability of the porous material in the tube. The
fluid pressure in (7) can be written in terms of equivalent
freshwater head using relation (1). With (6) and becauseoz/os is the cosine of the slope, the Darcy flux in a frac-
ture element can be written as
qfri ¼ �K fr0
ohfr0oxj
þ qfrr gj cosu
� �i; j ¼ 1; 2 ð8Þ
where gj is 0 in the horizontal direction and 1 along the
fracture incline. The incline of a fracture face is given by
u with u = 0� for a vertical face and u = 90� for a hor-izontal face. In the case of flow within fractures, a local
two-dimensional Cartesian coordinate system is as-
sumed. The freshwater hydraulic conductivity of the
fracture, K fr0 [L T�1], is derived from the parallel plate
model as
K fr0 ¼ ð2bÞ2q0g
12l0
ð9Þ
where (2b) [L] is the fracture aperture.
The application of Darcy�s law in fractures (8) re-
quires that the Reynolds number be smaller than 1 [2].
2.2.3. Governing equations
The governing equations for flow and transport in the
3D porous blocks are described first, followed by the
flow and transport equations in open fractures.
The equation that describes three-dimensional vari-
able-density flow under saturated conditions is [9]:
o
oxiK0
ij
oh0oxj
þ qrgj
� �� �¼ SS
oh0ot
i; j ¼ 1; 2; 3 ð10Þ
where fluid sources and sinks are not considered. Thespecific storage SS [L�1] accounts for both matrix and
fluid compressibility and is defined as [9]:
SS ¼ q0gðam þ /aflÞ ð11Þwhere am [M�1 L T2] and afl [M�1 L T2] are the matrix
and fluid compressibility, respectively.
Neglecting adsorption, radioactive decay and solutesources/sinks, the equation that governs solute transport
is the advective–dispersive flow equation in three dimen-
sions [1]:
o
oxi/Dij
ocoxj
� qic� �
¼ oð/cÞot
i; j ¼ 1; 2; 3 ð12Þ
The coefficients of the hydrodynamic dispersion ten-
sor Dij [L2 T�1] are given by Bear [1] as
/Dij ¼ ðal � atÞqiqjjqj þ atjqjdij þ /sDddij i; j ¼ 1; 2; 3
ð13Þwhere al [L] and at [L] are the longitudinal and trans-
verse dispersivity, respectively, dij [–] is the Kronecker
delta function, s [–] is matrix tortuosity and Dd
[L2 T�1] is the free-solution diffusion coefficient.
Flow and transport in an open discrete fracture take
place in two dimensions. Therefore, the corresponding
governing equations are defined in a local 2D coordinatesystem. The equation that governs variable-density flow
in fractures has been presented by several authors
[3,28,24,31]:
ð2bÞ o
oxiK fr
0
ohfr0oxj
þ qfrr gj cosu
� �� �� Sfr
S
ohfr0ot
� �þ qnjIþ � qnjI� ¼ 0 i; j ¼ 1; 2 ð14Þ
where the last two terms represent normal components
of the fluid flux across the boundary interfaces (I+ and
I�) that separate the fracture and the porous matrix.
In the conceptual model, fractures are idealized astwo-dimensional parallel plates. Therefore, both the
freshwater head, hfr0 , and the relative concentration, cfr,
are uniform across the fracture width.
The specific storage in the fracture, SfrS [L�1], can be
derived from (11) by assuming that the fracture is
incompressible, such that am = 0, and by setting its
porosity to 1:
SfrS ¼ q0gafl ð15ÞShikaze et al. [24] provide the equation for transport
in a discrete fracture as
ð2bÞ o
oxiDfr
ij
ocfr
oxj
� �� qfri
ocfr
oxi� ocfr
ot
� �þ XnjIþ � XnjI� ¼ 0 i; j ¼ 1; 2 ð16Þ
where Dfrij [L
2 T�1] is the hydrodynamic dispersion coef-
ficient of the fracture, defined by [30]:
Dfrij ¼ ðafr
l � afrt Þ
qfri qfrj
jqfrj þ afrt jqfrjdij þ Dddij i; j ¼ 1; 2
ð17Þ
where afr [L] is the fracture dispersivity. The last two
terms in Eq. (16) represent advective–dispersive loss or
gain of solute mass across the fracture–matrix interfaces
I+ and I� [28].
(0, Ly, Lz)
3
Ly
Lz
Lx
x
z
y
Sxy
4
12
Afeϕ
z
y
x=
(Lx, Ly, Lz)
(Lx, 0, 0)(0, 0, 0)
S: F(x, y, z) = constant
Sxz
H
Fig. 4. Geometry of an inclined 2D fracture element in three
dimensions.
T. Graf, R. Therrien / Advances in Water Resources 28 (2005) 1351–1367 1357
2.2.4. Finite element formulation of the buoyancy term in
a fracture
Frind [9] provides the finite element formulation of
the 2D variable-density flow equation in porous media
in the absence of fractures. The elements used in this
study are two-dimensional vertical undistorted rectan-gles. However, if fractures are present and assuming
the common node approach, the hydraulic head at the
fracture/matrix interface is identical in both media such
that the exchange terms qnjIþ and qnjI� in Eq. (14) van-
ish. In this case, the 2D flow equation in a porous matrix
as given in [9] and the 2D flow equation in a discrete
fracture given by (14) are mathematically identical. As
a consequence, Frind�s finite element formulationfor variable-density flow in 2D matrix elements can
also be used for density-driven flow in 2D fracture
faces.
Following Frind�s derivation, the finite element for-
mulation for Eq. (14) can be written as a semi-discrete
global matrix system in the compact form
H � h0 þ S � oh0ot
þ g ¼ f ð18Þ
where superscript ‘‘fr’’ is dropped for clarity. In (18), H
[L T�1] is the conductance or stiffness matrix, S [L] is the
fluid mass matrix, g [L2 T�1] is the body force vector and
f [L2 T�1] is the boundary flux vector. Vector g repre-sents density effects and is, therefore, of special interest
in this study. See [9] for details on the definition the
other matrices and vectors.
If 2D fracture faces are assumed, each of the four
arrays in (18) can be written as the sum of all the Nfe
elemental arrays, Nfe being the total number of fracture
elements in the grid. Following this, the fracture body
force vector, g, can be expressed as
g ¼Xfe
gfe ð19Þ
where gfe [L2 T�1] is the body force vector, written at thefracture elemental level. In a two-dimensional quadrilat-
eral element, whose sides coincide with the local coordi-
nate axis �x and �z, the entries gfei [L2 T�1] of vector gfe are
calculated after [9] as
gfei ¼Z Z
Afe
K fr0 �q
fer cosu
owfei
o�zd�xd�z i ¼ 1; 2; 3; 4 ð20Þ
where �qfer is the average relative density in the fracture
element (face) fe, wfei [–] is the value of the 2D approxi-
mation function in face fe at node i and Afe [L2] is the
surface area of fe. The double integral in (20) represents
the general mathematical expression of buoyancy in a
2D fracture face of any three-dimensional orientation.
However, the discretized inclined fracture can be a com-
bination of horizontal, vertical and inclined two-dimen-
sional elements. Integration of Eq. (20) is required toobtain the finite formulation of density effects for frac-
ture elements with arbitrary orientations, in order to
fully account for density effects in the entire fracture.
The right side of (20) can be integrated in two differ-
ent ways. First, the fracture weighting function is de-
fined in terms of local coordinates in the usual way
(e.g. for node 1) as wfe1 ¼ ðL�x � �xÞðL�z � �zÞ=ðL�x � L�zÞ, where
L�x [L] and L�z [L] are the element dimensions in the �x- and�z-direction, respectively (Fig. 4). With the derivative of
wfe1 , the integration in (20) is identical to that presented
by [9], resulting in the following coefficient for node 1:
gfe1 ¼ �K fr0 �q
fer cosu
L�x
2ð21Þ
which can be obtained likewise for the other nodes 2, 3
and 4.
The second, more general method first assumes a ver-
tical face, which will be rotated to match its real inclined
position. In this case of a vertical face, the cosine in (20)
is unity and the local coordinate axes of the face, �x and �z,coincide with the global coordinates, x and z (Fig. 4)
such that:
gfei ¼Z Z
Afe
K fr0 �q
fer
owfei
ozdxdz i ¼ 1; 2; 3; 4 ð22Þ
Unlike in the first method, the density term is now de-
fined over a vertical fracture element. If the quasi-verti-
cal face is rotated back to its original inclined position,
the buoyancy term (20) has to be integrated over the en-tire 2D inclined element area for an arbitrary face orien-
tation in 3D. However, the weighting function as well as
its derivative are 2D functions that are defined over a
surface defined in 3D space. Thus, a surface integral
calculus problem has to be solved where the function
f ðx; y; zÞ ¼ K fr0 �q
fer ðowfe
i =ozÞ is defined over the surface S
of the fracture face.
Following [32], the integral of a function f(x,y,z) overa surface S in space, described by the function
p
x
Surface F(x, y, z) = constant
Vertical projection orshadow of on acoordinate plane
Syz
R
S
Fig. 5. Projection of S on a coordinate plane [32].
1358 T. Graf, R. Therrien / Advances in Water Resources 28 (2005) 1351–1367
F(x,y,z) = constant (Fig. 5), can be calculated by evalu-
ating a closely related double integral over the vertical
projection or shadow of S on a coordinate plane in
the formZ ZSf ðx; y; zÞdS ¼
Z ZRf ðx; y; zÞ jrF j
jrF � pj dA ð23Þ
where R is the shadow region on the ground plane be-
neath surface S and p is a vector normal to R. This sur-
face integral can be directly evaluated only if a 1:1
mapping of S in the xy- or in the xz-plane exists. Then,
R could be Sxy or Sxz because both projections yield the
same result. The projection of S in the xz-plane is con-
sidered because a pseudo-vertical fracture element was
assumed.From Fig. 4, equation F(x,y,z) = constant of the sur-
face S, which defines the plane of the two-dimensional
fracture element, can easily be derived as Lzy � Lyz = 0.
Thus, a 1:1 mapping of S in both coordinate planes ex-
ists and, as a consequence, the integral on the right-hand
side of (23) can be evaluated and we have
S : F ðx; y; zÞ ¼ Lzy � Lyz ð24ÞrF ¼ 0 � iþ Lz � j� Ly � k ð25Þ
jrF j ¼ffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiL2y þ L2
z
qð26Þ
and with p = j, the unit vector in y-direction
jrF � pj ¼ jrF � jj ¼ Lz ð27Þ
Therefore, Eq. (23) becomes
Z ZSf ðx; y; zÞdS ¼
Z ZSxz
f ðx; y; zÞ
ffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiL2y þ L2
z
qLz
dxdz
ð28Þ
where dA = dxÆdz. With the function f ðx; y; zÞ ¼K fr
0 �qfer ðowfe
i =ozÞ, which must be integrated, the entries
of the elemental body force vector gfei from Eq. (20)
are given in the form
gfei ¼Z Lz
0
Z Lx
0
K fr0 �q
fer
owfei
oz
ffiffiffiffiffiffiffiffiffiffiffiffiffi1þ
L2y
L2z
sdxdz i ¼ 1; 2; 3; 4
ð29Þ
The elemental approximation function wfei is always
formulated as a function of local coordinates rather
than global ones. Therefore, the integral in Eq. (29)
has to be evaluated in the local coordinates �v. The re-
quired coordinate transformation is a rotation around
the x-axis by angle u (see Fig. 4) and can be written inthe matrix form
1 0 0
0 cosu � sinu
0 sinu cosu
264
375 �
x
y
z
8><>:
9>=>; ¼
�x
�y
�z
8><>:
9>=>; ð30Þ
Thus, we can write the derivatives
o�zoz
¼ cosu ð31Þ
ozo�z
¼ cosu ð32Þ
The integral of Eq. (29) is rewritten in terms of local
coordinates by first substituting the derivative by means
of the chain rule, leading to
owfei
oz¼ owfe
i
o�z� o�zoz
ð33Þ
and, second, by adjusting the elementary volume
following
dxdz ¼ det J � d�xd�z ð34ÞHere, the Jacobian matrix J [–] collapses to the simple
1 · 1 matrix
J ¼ ozo�z
� �ð35Þ
with determinant detJ given by Eq. (32). According toFig. 4, the approximation function for node 1 may be
expressed in local coordinates as
wfe1 ð�x;�zÞ ¼
1
LxHðLx � �xÞðH � �zÞ ð36Þ
with the spatial derivative
owfe1
o�z¼ �x� Lx
LxHð37Þ
where H [L] is the hypotenuse of the occurring triangle
in the yz-plane, given as H ¼ffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiL2y þ L2
z
q. Now use can
be made of Eqs. (31)–(35) and (37) to rewrite Eq. (29).
The elemental body force vector entry gfe1 can be written
in local coordinates as
gfe1 ¼Z H
0
Z Lx
0
K fr0 �q
fer
�x� Lx
LxH
� �cos2u
ffiffiffiffiffiffiffiffiffiffiffiffiffi1þ
L2y
L2z
s0@
1Ad�xd�z
ð38ÞFinally, a two-dimensional integration in Eq. (38)
directly yields the solution for node 1:
gfe1 ¼ �K fr0 �q
fer
LTG
2ð39Þ
T. Graf, R. Therrien / Advances in Water Resources 28 (2005) 1351–1367 1359
where the characteristic length LTG is a function of the
element geometry such that
LTG ¼ Lx �Lzffiffiffiffiffiffiffiffiffiffiffiffiffiffiffi
L2y þ L2
z
q ð40Þ
Note that solution (39) is identical to (21) because
Lx ¼ L�x and because the second factor in (40) is the
cosine of the fracture face incline, cosu ¼ Lz=ffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiL2y þ L2
z
q.
The repetition of steps (36)–(39) for nodes 2, 3 and 4
yields the following final form of the elemental body
force vector gfe for arbitrarily inclined two-dimensional
fracture elements.
gfe ¼ K fr0 �q
fer
LTG
2
�1
�1
1
1
8>>><>>>:
9>>>=>>>;
ð41Þ
where LTG is given by Eq. (40). The characteristics of
this length scale are:
(1) For a vertical fracture element, the calculated den-
sity effects reach a maximum. Solution (41)
becomes identical to that in [9] because LTG
becomes Lx:
limLy!0
LTG ¼ Lx
(2) For a horizontal fracture element, no density
effects occur and solution (41) becomes zero
because LTG vanishes:
limLz!0
LTG ¼ 0
(3) For every arbitrarily inclined fracture element, the
magnitude of the density effect will exceed zero
and will be smaller than the density effect in a ver-
tical fracture element:
0 < LTG < Lx
(4) For an inclined fracture element, which is not par-allel to the x-axis as shown in Fig. 4, but to the y-
axis as shown in Fig. 3, the x- and y-dimensions in
Eq. (40) are simply switched:
LTG ¼ Ly �Lzffiffiffiffiffiffiffiffiffiffiffiffiffiffiffi
L2x þ L2
z
q
2.3. Model verification
Variable-density flow and transport in porous media
was verified in two and three dimensions. All simula-
tions used implicit transport time weighting, as is com-
mon in other variable-density simulations, and fullupstream weighting as proposed by Folkovic and De
Schepper [10].
First, the Elder [7] salt convection problem was sim-
ulated to qualitatively test the model in two dimensions.
Kolditz et al. [14] point out that, for a coarse grid, the
central transport direction is downwards, whereas a fine
grid exhibits central upwelling. These observations were
confirmed by Prasad and Simmons [19] as well as in thepresent study using FRAC3DVS (Fig. 6).
Another code verification consisted in comparing the
Elder [7] results presented by Folkovic and De Schepper
[10] to those of FRAC3DVS. This verification is more
trustworthy than the one described in the previous par-
agraph because both numerical models (the Folkovic
and De Schepper [10] model and FRAC3DVS) use
the same numerical approach (control volume finite ele-ment method CVFE) as well as the same flow variable
(fluid pressure P). The governing flow equation for this
variable is given in the Appendix A. Folkovic and De
Schepper [10] carried out their numerical simulations
in the half domain of the symmetric Elder problem.
Interestingly, they found that an extremely fine grid
(32,768 nodes in the half domain) again exhibits central
downwelling, which was also discovered by Diersch andKolditz [5]. Their results are in very good visual
agreement with those from the FRAC3DVS model
(Fig. 7).
A new benchmark problem for variable-density
transport in 3D has been presented by Oswald and Kin-
zelbach [17]. This problem is based on the experimental
three-dimensional variable-density flow and solute
transport simulations in porous media conducted byOswald [16]. In these experiments, a 0.2 m · 0.2 m ·0.2 m closed box initially contained saltwater from the
bottom up to 8 cm, with the rest of the box filled with
freshwater. A constant freshwater recharge through
one upper corner of the box disturbed this stable layer-
ing of two miscible fluids. The concentration of the
mixed fluid versus time was measured at the discharging
open hole on the opposite side of the input location.Oswald [16] used two different initial concentrations
c01 = 0.01 (case 1) and c02 = 0.1 (case 2). The experimen-
tal results were numerically reproduced by Johannsen et
al. [13], who also present tabular data of the measured
concentrations versus time.
The FRAC3DVS model output was compared in
three dimensions with Oswald�s [16] experimental re-
sults, given in Johannsen et al. [13]. The physical param-eters given by Oswald and Kinzelbach [17] were used.
The first problem of the lower initial concentration
0.01 (case 1) was used because [13] showed that, in this
case, grid convergence is achieved with a relatively
coarse grid, whereas for case 2, the solution converged
only for a very fine grid, consisting of at least 274,625
grid points [13]. Good agreement between the experi-
mental results from [16], the numerical results from [5]and the FRAC3DVS model was obtained (Fig. 8). The
long-term results of this low density case more closely
2 years 2 years
4 years 4 years
10 years 10 years
Fig. 6. Results of the Elder problem for a coarse grid (left; 60 · 30 elements) and a fine grid (right; 120 · 40 elements) at 2, 4 and 10 yr simulation
time by Elder [7] [—; coarse grid], Kolditz et al. [14] [—; fine grid], Prasad and Simmons [19] [- �� -] and the present model [- -].
1 year 10 years
2 years 15 years
4 years 20 years
Fig. 7. Results of the Elder problem for an extremely fine grid (256 · 128 elements in the half domain) at 1, 2, 4, 10, 15 and 20 yr simulation time by
Folkovic and De Schepper [10] [—] and the present model [- -]. Shown are the 20%, 40%, 60% and 80% contours.
1360 T. Graf, R. Therrien / Advances in Water Resources 28 (2005) 1351–1367
resemble the experimental data than in [5]; however, dif-
ferences remain.
Variable-density flow in fractures was verified in a
two-step manner. First, the results of Shikaze et al.
0
0.01
0.02
0.03
0.04
0.05
0.06
0 50 100 150
time [min]
salt
mas
s fr
actio
n [%
] Experimental (Johannsen et al., 2002)
Numerical (the developed model)
Numerical (Diersch and Kolditz, 2002)
Fig. 8. Results of three-dimensional variable-density transport simu-
lations in porous media.
Fig. 10. Simulation geometry, boundary and initial conditions for
simulating density dependent flow and transport in fractured media.
Table 1
Model parameters used in fractured media studies
Parameter Value
Freshwater densitya (q0) 1000 kg m�3
Maximum fluid densitya (qmax) 1200 kg m�3
Fluid dynamic viscosityb (l) 3.545 · 104 kg m�1 yr�1
Fluid compressibilityb (afl) 4.42 · 10�25 kg�1 m yr2
Matrix compressibilityb (am) 2.51 · 10�24 kg�1 m yr2
Acceleration due to gravity (g) 9.75 · 1015 m yr�2
Tortuositya (s) 0.1
Matrix permeabilitya (jij) 10�15 m2
Matrix porosityc (/) 0.35
Matrix longitudinal dispersivitya (al) 0.1 m
Matrix transverse dispersivitya (at) 0.005 m
Fracture dispersivitya,d (afr) 0.1 m
Fracture aperturea (2b) 50 lmFree-solution diffusion coefficienta (Dd) 0.15768 m2 yr�1
a Ref. [24].b Ref. [14].c Ref. [9].d Ref. [30].
T. Graf, R. Therrien / Advances in Water Resources 28 (2005) 1351–1367 1361
[24] were used to verify density effects in vertical frac-
tures. With implicit transport time weighting, full up-
stream weighting of velocities and matrix porosity /= 0.35, which is used in [9], perfect agreement of the
output was obtained (results not shown).Second, variable-density transport in a fracture with
incline u = 45� was verified by comparing the results
from two different scenarios. In scenario 1, an inclined
fracture is discretized by only inclined faces. In a second
scenario, the inclined fracture consists of only vertical
and horizontal faces (Fig. 9), for which density effects
have already been successfully validated using the results
from [24]. In all simulations, we used a three-dimen-sional vertical slice with dimensions ‘x = 12 m,
‘y = 1 m and ‘z = 10 m as model domain. The left and
right boundaries are assumed to be impermeable,
whereas the top and bottom boundaries are specified
as constant equivalent head boundaries with zero con-
stant heads (Fig. 10). The contaminant source of con-
stant concentration, c = cL, overlies groundwater of
initial concentration, c = c0, where c0 = 0.0 < cL = 1.0.All simulations cover a time of 20 yr. Time step sizes
are kept constant at 0.2 yr. The input parameters for the
numerical simulations are shown in Table 1. These
parameters were held constant throughout all simula-
Fig. 9. Different discretization of the inclined fracture in scenario 1
and 2.
tions unless otherwise stated. It is assumed that the por-
ous matrix is isotropic and homogeneous throughout
and that the entire aquifer is completely saturated.
Grids of different discretization levels were generated
to investigate the adequate grid line density. The method
is called grid convergence study and it involves perform-
ing a simulation on successively finer grids. As the grid is
refined, the spatial discretization errors should asymp-totically approach zero, excluding computer round-off
errors.
Here, the grid at the lth level (l = 1,2, . . .) consists of480l2 identical square elements, which have the size
Dx = Dz = 1/2l m. Increasing grid levels correspond to
finer grids. Several simulations of scenario 1 were
performed at increasing grid levels and the tracer
breakthrough was monitored at the observation point(x = 6 m, z = 6 m) in the fracture as shown in Fig. 9.
Grid convergence was achieved for the grid of level 5
(Fig. 11), consisting of 12,000 square elements of size
Dx = Dz = 0.1 m. With this grid, the grid Peclet number
Peg = Dx/al becomes 1.0, satisfying the widely accepted
0
0.2
0.4
0.6
0.8
1 3 5 7 9 11 13 15
time [yr]
conc
entr
atio
n [--
]
grid5 grid4 grid3 grid2 grid1
Fig. 11. Scenario 1: grid convergence.
1362 T. Graf, R. Therrien / Advances in Water Resources 28 (2005) 1351–1367
criteria for neglecting numerical dispersion, Peg 6 2, as
well as oscillations, Peg 6 4.
It is remarkable that grid convergence was accom-
plished that easily, which is not obvious for convective
systems. This difficulty can be highlighted by consider-ing the Elder [7] problem, where the solute transport is
strongly controlled by convection. For this problem,
grid convergence is practically never achieved because
different qualitative results (i.e. central downwelling–
upwelling–downwelling) are obtained with different
spatial discretizations (i.e. coarse–fine–extremely fine).
Shikaze et al. [24] reached grid convergence by refining
the grid until the resulting concentration plots appearedunchanged (Shikaze, 2004, personal communication).
With the appropriate grid level 5, simulations of
scenario 1 and 2 were run. In order to account for the
longer path in the fracture of scenario 2, the fracture
velocities in this scenario were multiplied at each time
step with a correction factor. The ratio of the lengths
of the two fractures has to coincide with the ratio of
their average flow velocities, represented by the maxi-mum fracture velocity (see Fig. 13.4b). In the present
scenario 1
scenario 2
0
0.2
0.4
0.6
0.8
1
0
conc
entr
atio
n [--
]
Fig. 12. Results of the model verification for scenario 1 and 2: contour plots
observation point.
case of a 45�-inclined fracture, this ratio isffiffiffi2
p. The out-
put of the two simulations is shown in Fig. 12.
The model output from scenario 1 and 2 was objec-
tively compared by means of quantitative indicators
described by Prasad and Simmons [19]. The calculated
indicators are shown in Fig. 13. Using a quantitativeevaluation of model results also accounts for mass fluxes
(indicators 1 and 2) and for mass balance (5), in addition
to the conventional comparison of isochlors and break-
through curves (Fig. 12 left and right, respectively).
Figs. 12 and 13 clearly show that there is good agree-
ment between the two simulation results.
Fig. 13.4b can also be used to verify the Reynolds
number requirement, Re = qfrd/m < 1, for Darcy�s lawin fractures (Eq. (8)). The figure shows that the Darcy
flux in the fracture, qfr, does not exceed 10,000 m yr�1.
If the fracture aperture is chosen as the representative
microscopic length, d = (2b), and with the kinematic vis-
cosity given by m = l/q0, the Reynolds number is
0.01495. Thus, laminar flow as well as a linear relation-
ship between qfri and ohfr0 =oxj is ensured for all simula-
tions presented in Fig. 12 and Section 3.
3. Variable-density flow and transport in a single
inclined fracture
Variable-density flow simulations in a single fracture
have been conducted. For these simulations, the domain
geometry, as well as initial and boundary conditions areidentical to those shown in Fig. 10. All model parame-
ters correspond to those used by Shikaze et al. [24],
shown in Table 1. Similar to the code verification exam-
ples, constant time step sizes of 0.2 yr are used. Simula-
tions are first run for a 45�-inclined fracture, embedded
in a porous matrix. A demonstration of different buoy-
ancy effects in a single fracture of variable incline then
follows.
5 10 15 20
simulation time [yr]
scenario 1
scenario 2
(20% and 60%) at 8 yr simulation time and breakthrough curve at the
53.52 54.92
0
10
20
30
40
50
60
scenario 1 scenario 2tota
l mas
s tr
ansp
orte
d [y
r]
0
1
2
3
4
5
6
7
8
0 10 15 20
tota
lly s
tore
d m
ass
[kg]
0
2000
4000
6000
8000
10000
12000
0 10 15 20
max
. fra
c. v
el. [
m y
r-1]
2factor
(4b) (5)
0
2
4
6
8
10
0 10 15 20
Sher
woo
d nu
mbe
r [--]
0
0.01
0.02
0.03
0.04
0.05
0 10 15 20
simulation time [yr]
simulation time [yr]simulation time [yr]
simulation time [yr]
simulation time [yr]
max
. mat
rix v
el. [
m y
r-1] (4a)
0
2
4
6
8
10
0 10 15 20
pene
trat
ion
dept
h [m
] (3)
(2)(1)
5
5 5
5 5
Fig. 13. Results of the model verification with the quantitative parameters (1)–(5), applied to scenario 1 [—] and 2 [- -].
T. Graf, R. Therrien / Advances in Water Resources 28 (2005) 1351–1367 1363
For the first type of simulation, concentration dis-
tributions as well as velocity fields at 2, 4 and 10 yr
simulation time are shown in Fig. 14. The measured
concentrations versus time of this problem are given as
tabular data in Appendix B. After 2 yr, a convection cell
has formed on the left of the fracture near the source.
Flow along the fracture–matrix interface is mostly awayfrom the fracture. Note that the arrows do not represent
the magnitude of the velocity. Thus, solutes are trans-
ported from the fracture into the adjoining matrix
mainly by molecular diffusion and to a smaller degree
by advection. At 4 yr, a second cell has formed below
the fracture near the solute source. Both cells migrate
downwards into the aquifer. However, the cell above
the fracture has already moved further downwards be-cause it has been formed earlier. This more effective con-
vection cell forces the flow direction very close to the
fracture at the top of the domain to change directions.
As a consequence, the advective transport through the
upper boundary of the domain increases after 4 yr,
resulting in a rise of the Sherwood number as shown
in Fig. 13.1. Both convection cells are separated by the
high-permeability fracture, which, therefore, acts as a
barrier to convection. After 10 yr, some of the flow vec-
tors near the solute source have changed direction, thus
advectively transporting tracer from the matrix into the
fracture, and enhancing the buoyancy-induced flow
within the fracture. Therefore, convection in the porousmatrix appears to control the transport rate in an in-
clined fracture.
Several simulations were run with variable inclines
(u= 0�. . .70�) to investigate the transport behavior at
the limits of the fracture slope (0� and 90�). For all sim-
ulations, the grid had to be locally refined to ensure that
the fracture consists of only inclined faces. A value of
70� was the maximum incline used. The breakthroughcurves within the fracture at z = 6 m were monitored
and are shown in Fig. 15. The figure illustrates that,
for decreasing inclines, the observed buoyancy effect ap-
proaches the solution for a vertical fracture. Analo-
gously, the effect becomes less and less pronounced for
increasing inclines, finally being the solution for a
Fig. 14. Results of variable-density flow simulations after 2, 4 and 10 yr simulation time. Shown are the concentration distributions (left) and the
velocity field. Reddish colors represent a high solute concentration and blueish colors refer to low concentration.
0
0.2
0.4
0.6
0.8
1
0 2 4 6 8 10 12 14
time [yr]
conc
entr
atio
n [--
]
vertical 10 20 30 40 45 50 60 70
45°
70°
vertical
Fig. 15. Results of variable-density flow simulations with a single
variably inclined fracture: breakthrough curves at z = 6 m in the
fracture.
1364 T. Graf, R. Therrien / Advances in Water Resources 28 (2005) 1351–1367
horizontal fracture. Clearly, the two breakthrough
curves for the vertical and (almost) horizontal fracturecases are the envelope functions for the family of curves,
which can be described by c = cu(t). Interestingly, the
difference in concentration between two scenarios at a
given time is large for inclines which exceed 45� (close
to horizontal). Conversely, the concentration difference
is much smaller for almost vertical fractures. In Fig.
15, this phenomenon is indicated at 9 yr by two double
arrows. In both cases, two scenarios are comparedwhere the difference of the fracture incline is 10�. Thisphenomenon can be understood by remembering that
the buoyancy term in the Darcy equation (8) is weighted
with the cosine of the slope. The cosine function changes
weakly for small arguments because its derivative, the
negative sine, almost vanishes. On the contrary, the
change of the cosine function is relatively large for argu-
T. Graf, R. Therrien / Advances in Water Resources 28 (2005) 1351–1367 1365
ments close to 90�. Thus, the weight of the buoyancy
term in the Darcy equation changes weakly for almost
vertical fractures and changes greatly for almost hori-
zontal ones.
4. Summary and conclusions
An existing numerical model was modified to study
variable-density flow and transport in fractured-porous
media with inclined fractures. A general expression of
the body force vector, accounting for density effects,
was derived for fractures of any incline. Verification of
the model against a new experimental 3D test case forvariable-density transport in porous media showed very
good agreement between the experimental and model re-
sults. Variable-density flow in fractures was then tested
using two scenarios with a single 45�-inclined fracture.
In the first scenario, the fracture was discretized by in-
clined 2D elements, while in the second case, the fracture
consisted of horizontal and vertical elements. The frac-
ture velocities in this staircase-fracture were correctedwith the ratio of the two fracture lengths from scenario
2 and 1, respectively, in order to account for the longer
path in fracture 2. In order to rigorously test the code,
not only isochlors were compared, but also the break-
through curve on an observation point within the frac-
ture, the penetration depth of the 60% contour, global
mass fluxes and maximum velocities. Good agreement
between the results from the two scenarios wasobtained.
Simulations of variable-density flow in a porous ma-
trix with a 45�-inclined fracture show that two convec-
tion cells form at different times. Both cells grow with
time and migrate downwards into the aquifer. The
high-permeability fractures appear as barriers to convec-
tion. The velocity field at later simulation times indicates
that the two convection cells cause solutes to be trans-ported by advection from the porous matrix into the
fracture. Thus, convection within the matrix seems to
control density-driven flow in the fracture.
Several simulations in discretely fractured porous
media with a single variably inclined fracture are also
presented. The simulated density effects in an inclined
fracture approach those in fractures at the limits of the
incline. As the fracture becomes steeper, the resultsapproach the ones gained from a vertical fracture.
Correspondingly, results from virtually horizontal and
perfectly horizontal fractures are very similar. This
asymptotical behavior showed that the density effects
are calculated correctly at the fracture incline limits.
The foundation for further numerical modeling of
variable-density transport in more complex fracture net-
works was laid. The model can be used to study the on-set as well as the subsequent development of instabilities
in a fracture network, without being limited to only ver-
tical and horizontal fractures. Furthermore, neglecting
the influence of temperature effects on fluid density,
long-term predictions of contaminant migration in
fractured subsurfaces can be made on a large spatial
scale.
Acknowledgements
We thank the Canadian Water Network (CWN) as
well as the Natural Sciences and Engineering Research
Council of Canada (NSERC) for financial support of
this project. Author T.G. wishes to acknowledge both
the International Council for Canadian Studies (ICCS)and the German Academic Exchange Service (DAAD)
for providing a Postgraduate Scholarship stipend. We
are grateful to M.D. Graf for checking and improving
the English phrasing of the manuscript. The construc-
tive comments of four anonymous reviewers are
greatly appreciated and have helped improve the
manuscript.
Appendix A. Governing equations for the fluid pressure P
In order to reproduce the Elder [7] results given by
Folkovic and De Schepper [10], the FRAC3DVS
model had to be modified such that the same flow vari-
able, the fluid pressure P, can be employed to simulate
variable-density flow and solute transport in porousmedia.
The governing equation for variable-saturated vari-
able-density flow in porous media is given by Voss [33]
and has under fully saturated flow conditions the
three-dimensional form
o
oxibK0
ij
1
goPoxj
þ qgj
� �� �
¼ qSop
oPot
þ /oqoc
ocot
i; j ¼ 1; 2; 3 ðA1Þ
where b = q/qmax [–] and Sop [M�1 L T2] is the specificpressure storativity, given in [33] as
Sop ¼ ð1� /Þam þ /afl ðA2Þ
All other parameters have been defined in the text.
Moreover, the pressure gradient form of Darcy�s law
is
qi ¼ � jij
loPoxj
þ qggj
� �i; j ¼ 1; 2; 3 ðA3Þ
Lacking externally applied solute mass sources,
which is the case in the Elder [7] problem, the governing
equation for solute transport does not need to beadapted to the new flow variable P, and can be taken
as given by Eq. (12).
1366 T. Graf, R. Therrien / Advances in Water Resources 28 (2005) 1351–1367
Appendix B. Results of scenario 1 as tabular data
Table B.1
Simulation results of scenario 1: concentration breakthrough at z = 6 m in the fracture
t [yr] c [–] t [yr] c [–] t [yr] c [–] t [yr] c [–] t [yr] c [–]
0.0 0.00000
0.2 0.00000 4.2 0.30192 8.2 0.66246 12.2 0.76073 16.2 0.803484
0.4 0.00000 4.4 0.33476 8.4 0.67039 12.4 0.76362 16.4 0.805039
0.6 0.00000 4.6 0.36559 8.6 0.67783 12.6 0.76640 16.6 0.806557
0.8 0.00000 4.8 0.39437 8.8 0.68482 12.8 0.76908 16.8 0.808038
1 0.00000 5 0.42114 9 0.69141 13 0.77166 17 0.809485
1.2 0.00000 5.2 0.44599 9.2 0.69762 13.2 0.77415 17.2 0.810899
1.4 0.00002 5.4 0.46903 9.4 0.70349 13.4 0.77656 17.4 0.812281
1.6 0.00014 5.6 0.49037 9.6 0.70903 13.6 0.77888 17.6 0.813633
1.8 0.00071 5.8 0.51015 9.8 0.71428 13.8 0.78113 17.8 0.814955
2 0.00264 6 0.52847 10 0.71925 14 0.78331 18 0.816250
2.2 0.00749 6.2 0.54547 10.2 0.72398 14.2 0.78542 18.2 0.817518
2.4 0.01724 6.4 0.56124 10.4 0.72847 14.4 0.78747 18.4 0.818759
2.6 0.03342 6.6 0.57590 10.6 0.73274 14.6 0.78946 18.6 0.819976
2.8 0.05652 6.8 0.58953 10.8 0.73681 14.8 0.79139 18.8 0.821169
3 0.08578 7 0.60222 11 0.74069 15 0.79326 19 0.822339
3.2 0.11961 7.2 0.61404 11.2 0.74440 15.2 0.79508 19.2 0.823487
3.4 0.15615 7.4 0.62507 11.4 0.74795 15.4 0.79685 19.4 0.824614
3.6 0.19362 7.6 0.63537 11.6 0.75135 15.6 0.79858 19.6 0.825719
3.8 0.23092 7.8 0.64500 11.8 0.75461 15.8 0.80025 19.8 0.826805
4 0.26720 8 0.65402 12 0.75773 16 0.80189 20 0.827872
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