Research Article
Effects of the Grain Size on Dynamic Capillary Pressure and the
Modified Green–Ampt Model for Infiltration
Yi-Zhih Tsai ,
1Yu-Tung Liu,
2Yung-Li Wang,
1Liang-Cheng Chang,
3and Shao-Yiu Hsu
11Department of Bioenvironmental Systems Engineering, National Taiwan University, Taipei 10617, Taiwan 2Department of Water Resources Engineering and Conservation, Feng Chia University, Taichung 40724, Taiwan 3Department of Civil Engineering, National Chiao Tung University, Hsinchu 30050, Taiwan
Correspondence should be addressed to Shao-Yiu Hsu; syhsu@ntu.edu.tw
Received 20 April 2018; Accepted 12 July 2018; Published 26 August 2018 Academic Editor: Ching Hung
Copyright © 2018 Yi-Zhih Tsai et al. This is an open access article distributed under the Creative Commons Attribution License, which permits unrestricted use, distribution, and reproduction in any medium, provided the original work is properly cited. Darcy-scale capillary pressure is traditionally assumed to be constant. By contrast, a considerable gap exists between the measured and equilibrium capillary pressures when the same moisture saturation is considered with a high flow rate, and this gap is called the dynamic effect on the capillary pressure. In this study, downward infiltration experiments of sand columns are performed to measure cumulative infiltration and to calculate the wetting front depth and wetting front velocity in sands with different grain sizes. We estimate the equilibrium capillary pressure head or suction head at the wetting front using both the classical Green–Ampt (GAM) and modified Green–Ampt (MGAM) models. The results show that the performance of MGAM in simulating downward infiltration is superior to that of GAM. Moreover, because GAM neglects the dynamic effect, it systematically underestimates the equilibrium suction head in our experiments. We alsofind that the model parameters α and β of MGAM are affected by the grain size of sands and porosity, and the dynamic effect of the capillary pressure increases with decreasing grain size and increasing porosity.
1. Introduction
Infiltration involves gas and liquid flows in porous media and occurs during precipitation or when liquid contaminants leak underground or onto the soil surface. This contributes
to runoff generation, crop irrigation, and transport of
nutri-ents and contaminants. Infiltration is a main process in
sub-surface hydrology and plays a crucial role in geohazards, such
as landslides, flooding, and groundwater contamination.
Richards’ equation is the most general model to address such flows with spatially and temporally variable saturation [1, 2]. Nevertheless, computational time is an issue of numerically solving Richards’ equation in a large-scale simulation. There-fore, the simple one-dimensional Green–Ampt model (GAM) [3] is an attractive alternative [4, 5]. Actually, the GAM has been widely incorporated in large-scale hydrolog-ical processes and erosion models [6] such as HEC-HMS [7], WEPP [8], SWAT [9], and ANSWERS [10] models. However, describing the transient behavior during early
infiltration based on the GAM remains a challenging task.
The classical GAM for downward infiltration can be
expressed as an ordinary differential equation (ODE) [3, 11]:
θs− θi
Ks dlf
dt lf = hw+ sf+ lf, 1
whereθsis the saturated water content,θiis the initial water
content,Ksis the saturated hydraulic conductivity,lf is the
length of the porous medium with infiltrated liquid (the
wet-ting front depth), νf= dlf/dt is the wetting front velocity,
sf = Pc/ρg is the equilibrium suction head, Pc is capillary
pressure,ρ is the water density, g is the gravitational
acceler-ation, andhwis the ponding height. In the model, a wetting
front moves downward as a sharp moving boundary during
downward infiltration. The porous media above and below
the wetting front are assumed to have water saturated with
θsand unsaturated withθi, respectively. In addition, the air
pressure in the porous medium is assumed to be constant and, therefore, the viscous pressure drop due to the air
movement is neglected. The capillary pressurePc across the moving wetting front is commonly assumed to be constant and determined from the soil water retention curve [12, 13]. Nevertheless, during the past few decades, studies con-ducted under nonequilibrium conditions have indicated that the soil water retention curve may depend on the dynamics
of waterflow [14, 15]. Water content measured under
tran-sient flow conditions has been shown to be significantly
different from that measured under static and steady-state conditions [16–21]. Considering the soil water retention curve based on thermodynamics, Hassanizadeh and Gray [22], postulated the existence of a dynamic component in
the unsaturated water flow. This dynamic component
depends on both flow dynamics and the process of either
drainage or imbibition. In addition, studies conducting
col-umn experiments have shown that during downward in
filtra-tion, the water pressure head at the gas-water or liquid-liquid
interfaces changes as theflow velocity changes [11, 23–28].
The aforementioned studies suggest that the capillary pres-sure under dynamic conditions can be less than that under static conditions during infiltration. Therefore, infiltration can be better described by a GAM with a nonequilibrium
suction headsf.
The modified Green–Ampt model (MGAM) was first developed in Hsu and Hilpert [29]. They verified the model by the experimental data from upward infiltration [30], and
downward infiltration [25]. Hsu and Hilpert [29] showed
that the MGAM is better than the classical GAM at
describ-ing both transient capillary rise and downward infiltration in
dry sands. For downward infiltration, the MGAM can also be
expressed as an ordinary differential equation [11]:
θs− θi K dlf dtlf=hw+sf− γ dρgα η γ dlf dt β +lf, 2
whereγ is the interfacial tension, d is the grain size, α = αε
ϵ, θi is the lumped parameter related to a nondimensional
function (ε) of porosity ϵ and θi,α and β are model
parame-ters, andη is the dynamic viscosity of water. The additional
term γ/dρg α η/γ dlf/dt βis added into GAM to
con-sider the dynamic effect of capillary pressure.
The physical concept of the MGAM and the additional
parametersα and β are based on the theory of the pore-scale
dynamic contact angle. The upscaling of dynamic contact
angle to the dynamic effect of capillary pressure has been
derived and discussed in Hsu and Hilpert [29]. Based on the
studies of dynamic contact angle, β is in the range of 1/2
to 1/3, but the value ofα highly relies on the solid surface
structure [31–34].
Hsu et al. and Pellichero et al. [11, 26] showed that the MGAM approach can avoid the initial unphysical infinite rate of infiltration and better describe the experimental results than can the classical GAM for downward infiltration at an early stage in both dry and prewetted sand columns with varied initial water contents. Indications are that the
grain size and pore size distributions affect the dynamic effect
on the soil water retention curve [20, 35–37]. DiCarlo [36]
showed that when a saturation overshoot occurs during the
downward infiltration, the length of the gravitational finger-ing tips varies with the grain size and distribution. Hilpert [38] proposed a theory based on velocity-dependent capillary pressure that correctly predicts the degree to which the satu-ration overshoot depends on both the liquid contents and grain size. Hsu and Hilpert [29] pointed out that the model
parametersα and β in MGAM might be related to the
poros-ity and grain size. Based on (2), the dynamic effect on the suc-tion head should be inversely proporsuc-tional to the grain size. However, the effect of the grain size and pore size distribu-tion of the sand column on the nonequilibrium sucdistribu-tion head
as well as the model parametersα and β in (2) of the MGAM
have not yet been systematically investigated. Therefore, we
performed a series of infiltration experiment to
systemati-cally investigate the effect of the grain size of the sand column
on the nonequilibrium suction head as well as the model
parametersα and β.
In this study, the cumulative infiltration depths were
measured during a series of downward infiltration
experi-ments in dry sand columns with different grain sizes, subject
to different constant ponding heights. The remainder of this
paper is organized as follows. In Section 2, we describe our experimental method and preparation of the porous mate-rials. In Section 3, we describe the results of the experi-ments, and in Section 4, we compare the predictions from
classical GAM and MGAM as well as the values of fitting
parameters. We also discuss the effects of the grain size on
the dynamic capillary pressure and thefitting of the
equilib-rium suction head.
2. Experimental Setup
2.1. Experimental Material Properties and Grain Size Measurement. In this study, sands (glass beads) with four grain sizes (labeled B35, B60, B150, and B320) were used for our infiltration experiments. The sands had the same
shape, with a particle density of 2.5 g/cm3. Because glass
beads after conditioning hardly aggregate, we could exclude the influence of the aggregates on the observed dynamic cap-illary pressure. Moreover, the grain size distribution (GSD) of the sands was determined through sieve analysis (ASTM
C136) of eight different mesh screens.
2.2. Downward Infiltration Experiment. The infiltration
experiments were conducted using glassfilter columns (inner
diameter = 2.6 cm, depth = 60 and 30 cm, cross-section
area = 5.3 cm2). Based on Wang et al. [39], the sizes of the
fin-gering flow for downward infiltration in sands are mostly
ranged from 3 to 15 cm. Thefingering flow with a width of
less than 3 cm was only observed by Glass et al. [40]. In this study, our sand column with the inner diameter of 2.6 cm is
small enough to avoid 2Dfingering flows. All the sands were
conditioned by being rinsed with deionized water to remove
impurities and dried overnight in an oven at 100°C. We
packed sands B35, B60, and B150 into the 60 cm column and sand B320 into the 30 cm column. To achieve uniform packing, the sands poured into the column were maintained at a constant 3 cm distance between the supply funnel and the top of the sand packing. In addition, a rubber hammer was
used to tap the top of the sand in the column to obtain an even more homogeneous packing.
Figure 1 is a schematic representation of the experiment
setup. A Mariotte’s bottle was connected through Tygon
tub-ing and a valve to the sand column to maintain the hydraulic head. The bottle was placed on the top of an analytical balance (Sartorius TE1502S) to record the weight at 0.2 s intervals and automatically send the data to a computer. When the valve was opened, the water in the Mariotte’s bottle flowed into the column packed with dry sand, infiltrated the sand and reached the bottom of the column. The weight change mea-sured by the analytical balance was used to calculate the cumulative infiltration and infiltration rate. All infiltration experiments in this study were conducted in triplicate.
2.3. Saturated Hydraulic Conductivity (Ks) Measurement.
Saturated hydraulic conductivity (Ks) is an important
param-eter of the GAM, as it dparam-etermines theflow rate of water in the
saturated soil. Ks in this study was determined by the
constant-head method. The measurement procedure was the same as that for the infiltration experiment previously described. Following the infiltration experiments, the sand
in the column was at saturation, and theflow rate gradually
reached equilibrium. We measured the equilibrium
infiltra-tion rate, and Kswas estimated based on Darcy’s law:
Ks=QL
Ah, 3
whereQ is theflow rate, L is the length of the sand column, A
is the total cross-section area, andh is the constant hydraulic
head. The flow rate value was obtained by calculating the
weight change of water per unit time.
3. Results
3.1. Grain Size Distribution of Experimental Materials. Figure 2 shows the grain size distributions of the sands. Sand B35 was the coarsest in grain size, ranging from 2 to
7 × 10−2cm and was followed in order by B60 (distributed
between 1 and 6 × 10−2cm), B150 (ranging from 5 × 10−3to
2.3 × 10−2cm), and B320 (which had the finest grain size
and was distributed between 1 × 10−4and 2 × 10−2cm).
The curves in Figure 2 are plotted based on a grain size distribution equation provided by Fredlund et al. [41]. We used the same equation to calculate the geometric mean grain
size (d50). Table 1 shows the geometric mean grain sizes of
sands B35 (4.51 × 10−2cm), B60 (3.48 × 10−2cm), B150
(1.38 × 10−2cm), and B320 (1.3 × 10−3cm).
The sands were uniform. Specifically, the uniformity coefficients of sands B35, B60, B150, and B320 were 1.33, 1.46, 1.55, and 3.85, respectively. In the discussion that
fol-lows, we used d50to quantify the effect of grain size on the
infiltration model and dynamic capillary pressure.
3.2. Results of Infiltration Experiments. Table 1 shows the
measured porosity, bulk density, and saturated hydraulic
conductivity. In each of the 36 infiltration replicate
experi-ments, we controlled the bulk density and porosity of the soil column. The average bulk density of sand B35 column was
1.36 g/cm3and the average porosity was 0.46 cm3/cm3. The
bulk density of sand B60 was 1.42–1.43 g/cm3, B150 was
1.38–1.39 g/cm3, and B320 was 1.33–1.36 g/cm3. The
poros-ity of sands B60, B150, and B320 was 0.43, 0.45, and
0.47 cm3/cm3, respectively.
Under the assumption of GAM, the sand has a water
content θ = θsbehind the wetting front and an initial water
content θi ahead of the front. Mobile water content (Δθ)
indicates the moisture change θs− θi at the wetting front
and can be estimated from the total cumulative infiltration
and total volume of the sand column, that is, Δθ = Ftotal/
Vtotal [11]. In our study, the Δθ of sand B35 column was
obtained from 0.42 to 0.44 cm3/cm3, B60 from 0.39 to
0.41 cm3/cm3, B150 from 0.40 to 0.42 cm3/cm3, and B320
from 0.39 to 0.44 cm3/cm3.
The results of the saturated hydraulic conductivity from additional experiments show that B35 had the largest
value, followed by B60, B150, and B320, at 1.84–
1.97 × 10−1, 6.42–6.53 × 10−2, 1.16–1.42 × 10−2, and 0.8– 1.1 × 10−3cm/s, respectively. Mariotte′s bottle Analytical balance Computer Valve Column Wetting front
Figure 1: Schematic of the experimental setup for the downward infiltration experiments. 100 90 80 70 60 50 40 30 20 10 0 C u m u la ti ve p er cen ta ge b y w eig h t passin g (%) 10−1 10−2 10−3 10−4 Particle diameter (cm) B150 B320 B35 B60
Figure 2: Grain size distribution curves of sands B35, B60, B150, and B320.
We used the analytical balance to measure the mass
(mw) of water infiltrating the sand column. In addition, the
cumulative infiltration (F) was calculated from the mass
(mw), water density (ρ), and soil column cross-sectional area
(A), such that F = mw/ρA. We plotted the relationship
betweenF and time t according to different water ponding
heights and soil sizes. Figure 3 shows F versus t in our
experiments. Each plotted point represents the average result of three replicate experiments. However, one of the infiltration experiments of soil B320 column at a water ponding height of 20 cm failed because of water leakage, a fact that was not mentioned in our subsequent discussion.
Figures 3(a)–3(d) clearly show that F increased as the water
ponding height increased.
Table 1: Geometric mean grain size, porosity, bulk density, and saturated hydraulic conductivity for column experiments with different ponding heights.
Materials Geometric mean grain size, d50× 10−4(cm) Water ponding height, hw(cm) Bulk density, ρb(g·cm−3) Porosity,
ϵ (cm3·cm−3) Mobile water content,Δθ (cm3·cm−3)
Saturated hydraulic conductivity, Ks× 10−2(cm·s−1) B35 10 1.36 ± 0.006 0.46 ± 0.003 0.44 ± 0.011 19.68 ± 0.683 451 20 1.36 ± 0.002 0.46 ± 0.001 0.42 ± 0.006 18.35 ± 0.132 40 1.36 ± 0.017 0.46 ± 0.007 0.43 ± 0.006 18.37 ± 1.591 B60 10 1.43 ± 0.003 0.43 ± 0.001 0.41 ± 0.014 6.53 ± 0.202 348 20 1.42 ± 0.005 0.43 ± 0.002 0.39 ± 0.003 6.42 ± 0.079 40 1.42 ± 0.008 0.43 ± 0.003 0.39 ± 0.003 6.50 ± 0.393 B150 10 1.38 ± 0.004 0.45 ± 0.002 0.40 ± 0.001 1.21 ± 0.024 138 20 1.38 ± 0.007 0.45 ± 0.003 0.40 ± 0.005 1.16 ± 0.055 40 1.39 ± 0.000 0.45 ± 0.000 0.42 ± 0.021 1.42 ± 0.391 B320 10 1.36 ± 0.004 0.46 ± 0.002 0.39 ± 0.007 0.08 ± 0.003 13 20 1.34 ± 0.013 0.47 ± 0.005 0.44 ± 0.040 0.11 ± 0.026 40 1.33 ± 0.006 0.47 ± 0.002 0.42 ± 0.036 0.10 ± 0.028 25 20 15 10 5 0 0 20 40 60 80 Time (s) C u m u la ti ve infil tra tio n (cm) 25 20 15 10 5 0 0 50 100 150 200 250 Time (s) (a) (b) (c) (d) C u m u la ti ve infil tra tio n (cm) Time (s) 0 200 400 600 800 1000 C u m u la ti ve infil tra tio n (cm) 30 25 20 15 10 5 0 hw = 10 cm hw = 20 cm hw = 40 cm Time (s) 0 500 1000 1500 2000 2500 C u m u la ti ve infil tra tio n (cm) 14 12 10 8 6 4 2 0
3.3. Wetting Front Depth and Velocity versus Water Ponding
Height and Grain Size. Wetting front depth lf can be
cal-culated fromF andΔθ, such that lf=F/Δθ. Figure 4 shows
lf versus t in our experiments. In general, the lf
monoto-nously increased with t. In addition, water ponding height
hw= 40 cm had the largest lf value at the same time,
followed byhw= 20 cm andhw= 10 cm. For different grain
sizes, the wetting front of B35 with the largest grain size and
fastest infiltration rate spent 55–80.8 s to arrive lf= 60 cm,
B60 spent 125–217.6 s, and B150 spent 597.2–980 s. Finally, the wetting front of B320 with the smallest grain size and
slow-est infiltration rate spent 2040–2430 s to arrive lf = 30 cm.
We divideddlf bydt to obtain the wetting front velocity
νf and plotted the relationship ofνf andt in Figure 5. To
compare the wetting front velocities in different experiments
witht, we normalized the X axis through t divided by the
infiltration end time tie . Figure 5 showsνfversus
standard-ized time t/tie . We can see that νf was the fastest at the
beginning of infiltration, gradually decreased with t, and finally approached an equilibrium value. Regardless of the
water ponding height,νfincreased as the grain size increased.
The main purpose of this study is to examine the
relationship between flow velocity and capillary pressure
during transient infiltration. The combination of ponding
depths and grain sizes can lead to a range of flow rates
and front velocities for examining our hypothesis. In
addition, our experimental results shown in Figures 4 and
5 confirm that our experimental design in accord with the
basic physical assumptions of infiltration theory and the
GAM. It implies that thefingering flow did not occur
dur-ing our experiments.
3.4. Infiltration Simulation of GAM and MGAM. In this
study, experimental data were modeled by GAM and MGAM. We used a MATLAB implementation of ODE solvers to provide a numerical solution of GAM (1) and MGAM (2) in downward infiltration conditions. GAM
required only a parameter sf for simulation, whereas other
parametersKs andΔθ were inputted as fixed values (listed
in Table 1). Parameters used by MGAM included sf,α, β,
d, Ks, andΔθ, where KsandΔθ were inputted as fixed values
(listed in Table 1). Here, grain size d was represented by
the geometric mean grain size (d50).
The fitting parameters were inversely determined from
the measured data using a MATLAB nonlinear fitting
function. The nonlinear fitting function uses a
Levenberg-Marquardt nonlinear least squares algorithm to solve bound-constrained optimization problems [42]. MATLAB
nonlinear fitting function must specify the initial value of
sf,α, β, and d. Based on the studies of Hsu et al. [11] and
Pellichero et al. [26], we setα = 100 and β = 0 3 as the initial
values for modelfitting. The initial value of d of sands B35,
60 50 40 30 20 10 0 W et tin g f ro n t dep th (cm) 0 20 40 60 80 Time (s) 60 50 40 30 20 10 0 W et tin g f ro n t dep th (cm) 0 50 100 150 200 Time (s) (a) (b) (c) (d) 60 50 40 30 20 10 0 W et tin g f ro n t dep th (cm) 0 200 400 600 800 Time (s) hw = 10 cm hw = 20 cm hw = 40 cm 30 25 20 15 10 5 0 W et tin g f ro n t dep th (cm) 0 500 1000 1500 2000 Time (s)
Figure 4: Wetting front depth of sand versus time: (a) B35, (b) B60, (c) B150, and (d) B320. The column length of sands B35, B60, and B150 was 60 cm and of sand B320 was 30 cm.
B60, B150, and B320 was d50= 4 51 × 10−2, 3.48 × 10−2,
1.38 × 10−2, and 1.3 × 10−3cm, respectively. The initial value
ofsf was obtained by
sf =
2γ cos φ
rρg , 4
whereγ is interfacial tension (in which the surface tension of
water and air isγ = 7 2 × 10−2N/m),g is gravity acceleration
(g = 9 81 m/s2),ρ is water density (ρ = 1000 kg/m3),φ is
con-tact angle, and r is effective pore radius. In this study, the
contact angle was φ = 30°; this was the static contact angle
of quartz and water suggested by Friedman [43]. We used the empirical formula of Glover and Walker [44] to convert
grain size d into effective pore size r :
r = d
2 8/3 × 1 52/8ϵ2×1 5, 5
whereϵ is porosity. The aforementioned initial values were
substituted in (1) and (2) to simulate GAM and MGAM for
downward infiltration, respectively.
The results of infiltration simulation of GAM and
MGAM are shown in Figure 6, and the modelfitting
param-eters are listed in Table 2. In Figure 6, the black circles are the wetting front depths, which were calculated from the
measured values of mw. The remaining four curves show
the simulation results of GAM and MGAM. The orange-dotted curve (GAM) was plotted by GAM with the
calcu-lated sf based on (4). The yellow-dashed curve (MGAM)
was simulated by MGAM with α = 100, β = 0 3, sf (which
was calculated by (4)), andd = d50. The purple-dashed curve
(optimized GAM) used the nonlinearfitting method to
sim-ulate downward infiltration by GAM with sf as a fitting
parameter. Finally, the green-solid curve (optimized MGAM)
was represented by MGAM with α, β, sf, andd as fitting
parameters. Both the purple-dashed and green-solid curves
with fitting parameters showed better simulation results;
these curves could approach the black circles of the wetting
front depth. The orange-dotted curve with afixed sf was
far-thest from the black circles, followed by the yellow-dashed
curve withfixed α, β, sf , and d in the middle. This indicates
that the performance of MGAM with multiparameters for
simulating downward infiltration was superior to that of
the classical GAM.
Regardless of the grain size of the sand, the optimized
GAM and optimized MGAM with the fitting parameters
had good simulation results. For GAM and MGAM with
no fitting parameters, the smaller the grain size, the more
the simulation results deviated from the black circles, partic-ularly the sand B320.
Table 2 shows that two of thefitting suction heads sf of
sand B35 based on GAM were negative. Because the grain 4 vf (cm/s) 3 2 1 0 0 0.2 0.4 0.6 0.8 1 t/tie 4 vf (cm/s) 3 2 1 0 0 0.2 0.4 0.6 0.8 1 t/tie (a) (b) 6 vf (cm/s) 4 2 0 0 0.2 0.4 0.6 0.8 1 t/tie (c) B35 B60 B150 B320
Figure 5: Wetting front velocity of sands B35, B60, B150, and B320 under ponding height of: (a) hw= 10 cm, (b)hw= 20 cm, and (c) hw= 40 cm.
size of the B35 was larger than that of other sands, the
equi-libriumsf was relatively small or even close to zero (Figure 7
and Table 2). Nevertheless, to have a negative suction head
for a sand column packed with glass beads is still abnormal.
It implies that the sf was underestimated by using classical
GAM during a downward infiltration with high wetting front 60 50 40 30 20 10 0 W et tin g f ro n t dep th (cm) 0 10 20 30 40 50 60 70 80 Time (s) hw = 10 cm B35 60 50 40 30 20 10 0 W et tin g f ro n t dep th (cm) 0 10 20 30 40 50 60 70 Time (s) hw = 20 cm 60 50 40 30 20 10 0 W et tin g f ro n t dep th (cm) 0 10 20 30 40 50 Time (s) (a) (b) (c) (d) (e) (f) (g) (h) (i) (j) (k) (l) hw = 40 cm 60 50 40 30 20 10 0 W et tin g f ro n t dep th (cm) B60 0 50 100 150 200 Time (s) 60 50 40 30 20 10 0 W et tin g f ro n t dep th (cm) 0 20 40 60 80 100 120 140 160 Time (s) 60 50 40 30 20 10 0 W et tin g f ro n t dep th (cm) 0 20 40 60 80 100 120 Time (s) 60 50 40 30 20 10 0 W et tin g f ro n t dep th (cm) 0 200 400 600 800 Time (s) B150 60 50 40 30 20 10 0 W et tin g f ro n t dep th (cm) 0 100 200 300 400 500 600 700 800 Time (s) 60 50 40 30 20 10 0 W et tin g f ro n t dep th (cm) 0 100 200 300 400 500 600 Time (s) 0 500 1000 1500 2000 Time (s) Optimized GAM Optimized MGAM 30 25 20 15 10 5 0 W et tin g f ro n t dep th (cm) Measured data GAM MGAM B320 0 500 1000 1500 2000 Time (s) 30 25 20 15 10 5 0 W et tin g f ro n t dep th (cm) 0 500 1000 1500 2000 Time (s) 30 25 20 15 10 5 0 W et tin g f ro n t dep th (cm)
velocity. According to Chow et al. [12], thesf is distributed from 0.97 cm (0.0097 m) to 156.5 cm (1.565 m) from sand to clay. From the grain size distribution in Figure 2, the
tex-ture class of B320 can be classified as silt loam. Its sf value
ranges from 2.92 cm (0.0292 m) to 95.39 cm (0.9539 m). However, theoretical values of sf based on (4) are over 2 m.
The sf value for sand B320 is larger than that from
Chowet al. [12], but it should still be in the range of silt loam or soils slightly smaller than silt loam for practical problems. The performances of GAM and MGAM were evaluated using root mean square error (RMSE). For each simulation,
the difference between the measured wetting front depth
(lf(m)) and the calculated wetting front depth (lf(p)) was
expressed in RMSE as:
RMSE = ∑ N i=1 lf m − lf p 2 N , 6
where N is the number of observed samples. By statistically verifying RMSE, we could evaluate the reliability of the model simulation; when the RMSE was small, the model was more reliable. The results of RMSE for infiltration simulation of GAM and MGAM are listed in Table 2. In general, the RMSEs of most MGAMs (0.001–0.008) in this study were less than those of GAMs (0.002–0.011), indicating that the simulation results of MGAM were superior to those of GAM. Except for two sets of simulation results for B60 and B320, the RMSE of GAM was smaller than that of MGAM. Fortunately, the RMSE of these two sets of results were also very small, which meant that the performance of MGAM was also good.
4. Discussion
4.1. Relationship between Wetting Front Suction Head sf
and Grain Size. The relationship between the suction head and grain size can be linked by using (4) and (5). Figure 7 shows the relationship between the grain sizes of the sand columns and the equilibrium suction heads estimated by GAM and MGAM. The solid line in Figure 7 shows the the-oretical relationship based on (4) and (5) between the grain Table 2: Model parameters and RMSE of GAM and MGAM for downward infiltration simulation.
Materials hw(cm) GAM MGAM sf(m) RMSE sf (m) α β d (×10−4cm) RMSE B35 10 0.011 0.007 0.105 86.138 0.305 425 0.004 20 −0.009 0.011 0.094 93.316 0.297 456 0.008 40 −0.052 0.009 0.09 100.741 0.283 442 0.006 B60 10 0.053 0.002 0.112 85.391 0.339 361 0.003 20 0.025 0.005 0.133 98.828 0.3 351 0.002 40 0.015 0.007 0.135 93.037 0.29 361 0.004 B150 10 0.134 0.008 0.326 97.797 0.288 138 0.003 20 0.147 0.004 0.323 98.817 0.3 138 0.001 40 0.099 0.006 0.31 98.585 0.291 137 0.002 B320 10 0.528 0.003 1.063 95.888 0.335 16 0.003 20 0.467 0.002 1.007 97.124 0.335 17 0.004 40 0.279 0.009 1.496 109.98 0.305 13 0.002 2 1.5 1 0.5 0 0 200 400 600 Grain size (×10−4 cm) Sf (m)
Estimated from (4) with contact angle = 30° Estimated from (4) with contact angle = 63° Estimated from (4) with contact angle = 84° B35 from MGAM B60 from MGAM B150 from MGAM B320 from MGAM B35 from GAM B60 from GAM B150 from GAM B320 from GAM
Figure 7: Wetting front suction head sf versus grain size. In all sands,sf from MGAM was larger than sf from GAM. The solid curve estimatessf from a static contact angle of 30°, the dotted line represents the best contact angle (63°) withsf from MGAM, and the dashed-dotted line represents the contact angle = 84°with sf from GAM.
sizes of the sand columns and the equilibrium suction heads with the assumed effective contact angle between air, water,
and the glass bead of 30°. Using the same equations, we
determined the effective pore radius and contact angles by fitting the effective contact angle to the grain size and the determined equilibrium suction heads. The dashed lines in
Figure 7 show the fitted relationship between grain sizes
and the equilibrium suction heads estimated by GAM and
MGAM with the fitted effective contact angle of 84° and
63°, respectively.
The equilibrium suction heads estimated by the GAM were systematically lower than those estimated by the MGAM. Consequently, the effective contact angle estimated by the GAM was also systematically greater than that by
the MGAM. The overestimated effective contact angle from
GAM was because we neglected the dynamic effect when
estimating the suction head. The effective contact angle
esti-mated by GAM was the average dynamic contact angle dur-ing the infiltration process. Nevertheless, the contact angle
(63°) estimated by MGAM was still greater than that (30°)
measured in previous studies, even when the dynamic effect was considered. One explanation for this is related to the contact angle hysteresis: the contact angle no longer corre-sponds to the static equilibrium angle but is larger when the liquid is advancing and smaller when the liquid is
reced-ing [45]. In general, durreced-ing the infiltration, the water
advances the air in the sand. Therefore, the contact angle during the infiltration should be in the form of an advancing contact angle, which is commonly greater than the equilib-rium contact angle.
4.2. MGAM Fitting Parameters for Dynamic Capillary Pressure. Hsu and Hilpert [29] pointed out that the parame-tersα and β in the MGAM are related to the dynamic effect on the capillary pressure, and their values might not be the same for different initial water contents, porosities, and grain
sizes. Figure 8 shows two trends in which thefitted α is
pro-portional to the porosity and inversely propro-portional to the grain size. From the empirical relationship proposed by
Stauffer [20] relating the dynamic coefficient to measurable
porous media andfluid properties, the equation suggests that
the dynamic effects would be greater for fine-grained soil with high air entry pressure and high porosity. Camps-Roach eat al. [35] observed that the dynamic coefficient sta-tistically increases as the grain size decreases. Therefore, our fitted values of the parameters were consistent with those of the aforementioned studies.
Limited numbers of Darcy-scale studies focus on
deter-mining the β values in sand. Weitz et al. [28] yielded β =
0 5 ± 0 1 for water displacing decane in a glass bead column.
Hsu and Hilpert [29] tested a range ofβ values from 1/5 to 1
based on the studies of pore-scale dynamic contact angles
on flat surfaces and in circular capillary tubes, which can
110 100 90 80 aˆ 0 100 200 300 400 500 Grain size (×10−4 cm) B60 B35 B150 B320 Y = −0.02X + 101.06 (a) 110 100 90 80 aˆ B60 B35 B150 B320 0.42 0.44 0.46 0.48 Porosity (cm3/cm3) Y = 189.09X + 11.32 (b)
Figure 8: MGAM parameter α versus (a) grain size and (b) porosity.
0.34 0.32 0.3 0.28 0.26 0.24 B320 B150 B60 B35 0 100 200 300 400 500 Grain size (×10−4 cm) 훽 Y = 0.3
Figure 9: MGAM parameter β versus grain size. The fitted β was approximately 0.3.
be described by cosφeq− cos φdyn=αCaβ [33, 34, 46]. The best β value was approximately 0.31 for the experiments performed by Geiger and Durnford [25]. Pellichero et al.
[26] showed thatβ = 0 3 resulted in the best fit in downward
infiltration experiments with the same sand but varying
ponding heights. The sameβ value also worked well in
sim-ilar experiments but with various initial water contents [11].
In this study, β was set as one of the fitting parameters.
Figure 9 shows that thefitted β was approximately 0.3, and
the error bars overlapped for most grain sizes except for those
of B320, which had the highestβ value (up to 0.34) with the
smallest grain size. Nevertheless, the value of thefitted β in
this study agreed with the values derived or determined from the aforementioned Darcy and pore-scale studies. We con-firmed again that 0.3 is a universal value for β for Darcy’s scale sand experiments.
5. Conclusions
We performed a series of downward infiltration experiments and compared the predictions derived from classical GAM
and MGAM as well as the values of fitting parameters. In
this study, cumulative infiltration monotonously increased
with time, and a greater water ponding height showed more
cumulative infiltration. This kind of result was also reflected
in the wetting front depth. Furthermore, the sand column
with smaller grain size had a lower infiltration rate and
wetting front velocity, and a greater amount of time was spent on infiltration. Regarding the model simulation, the RMSEs of MGAM were less than those of GAM, indicating that the performance of MGAM with multiparameters for simulating downward infiltration was superior to that of the classical GAM.
Because the classical GAM ignores the dynamic effect on
estimating the suction head, the effective contact angle
esti-mated by GAM was systematically greater than that by MGAM, meaning that the equilibrium suction from GAM was systematically less than that from MGAM. Moreover, the contact angle is typically in the form of an advancing one during infiltration. Therefore, the equilibrium contact angle estimated by MGAM was greater than the intrinsic
con-tact angle. In addition, thefitted α was proportional to the
porosity and inversely proportional to the grain size in our
study, indicating that the dynamic effect of capillary pressure
increased with decreasing grain size and increasing porosity.
Furthermore, thefitted β was approximately 0.3, which is
con-sistent with the values obtained from most of Darcy’s and pore-scale studies. This study confirmed that 0.3 can be the
universal value ofβ for Darcy-scale sand experiments.
Data Availability
The data used to support thefindings of this study are
avail-able from the corresponding author upon request.
Conflicts of Interest
The authors declare that there is no conflict of interest regarding the publication of this paper.
Acknowledgments
The authors thank the editors and anonymous referees for their thoughtful comments and suggestions. The authors also want to thank the Ministry of Science and Technology
(MOST), Taiwan, for financially supporting this research
under Grant MOST 106-2628-M-002-009-MY3 and MOST 106-2923-E-009-001-MY3.
References
[1] D. A. Barry, J.-Y. Parlange, G. C. Sander, and M. Sivaplan, “A class of exact solutions for Richards' equation,” Journal of Hydrology, vol. 142, no. 1–4, pp. 29–46, 1993.
[2] G. Sposito,“Recent advances associated with soil water in the unsaturated zone,” Reviews of Geophysics, vol. 33, no. S2, pp. 1059–1065, 1995.
[3] W. H. Green and G. A. Ampt,“Studies on soil physics part I– the flow of air and water through soils,” Journal of Agricul-tural Science, vol. 4, pp. 1–24, 1911.
[4] S. M. Hsu, C.-F. Ni, and P.-F. Hung,“Assessment of three infil-tration formulas based on modelfitting on Richards equation,” Journal of Hydrologic Engineering, vol. 7, no. 5, pp. 373–379, 2002.
[5] G. Liu, J. R. Craig, and E. D. Soulis, “Applicability of the Green-Ampt infiltration model with shallow boundary condi-tions,” Journal of Hydrologic Engineering, vol. 16, no. 3, pp. 266–273, 2011.
[6] A. Van den Putte, G. Govers, A. Leys, C. Langhans, W. Clymans, and J. Diels,“Estimating the parameters of the Green–Ampt infiltration equation from rainfall simulation data: why simpler is better,” Journal of Hydrology, vol. 476, pp. 332–344, 2013.
[7] A. D. Feldman, “Hydrologic modeling system HEC-HMS: technical reference manual,” in US Army Corps of Engineers, Hydrologic Engineering Center, 2000.
[8] J. M. Laflen, W. Elliot, D. Flanagan, C. Meyer, and M. Nearing, “WEPP-predicting water erosion using a process-based model,” Journal of Soil and Water Conservation, vol. 52, no. 2, pp. 96–102, 1997.
[9] P. Tuppad, K. R. Douglas-Mankin, T. Lee, R. Srinivasan, and J. G. Arnold, “Soil and water assessment tool (SWAT) hydrologic/ water quality model: extended capability and wider adoption,” Transactions of the ASABE, vol. 54, no. 5, pp. 1677–1684, 2011. [10] F. Bouraoui and T. A. Dillaha,“ANSWERS-2000: runoff and sediment transport model,” Journal of Environmental Engi-neering, vol. 122, no. 6, pp. 493–502, 1996.
[11] S.-Y. Hsu, V. Huang, S. Woo Park, and M. Hilpert,“Water infiltration into prewetted porous media: dynamic capillary pressure and Green-Ampt modeling,” Advances in Water Resources, vol. 106, pp. 60–67, 2017.
[12] V. T. Chow, D. R. Maidment, and L. W. Mays, Applied Hydrol-ogy, McGraw-Hill, 1988.
[13] S. P. Neuman,“Wetting front pressure head in the infiltration model of Green and Ampt,” Water Resources Research, vol. 12, no. 3, pp. 564–566, 1976.
[14] R. S. Mokady and P. F. Low,“The tension-moisture content relationship under static and dynamic conditions1,” Soil Sci-ence Society of America Journal, vol. 28, no. 4, 1964. [15] G. C. Topp, A. Klute, and D. B. Peters, “Comparison of
steady-state, and unsteady-state methods1,” Soil Science Society of America Journal, vol. 31, no. 3, p. 312, 1967. [16] E. Diamantopoulos and W. Durner, “Dynamic
nonequilib-rium of waterflow in porous media: a review,” Vadose Zone Journal, vol. 11, no. 3, 2012.
[17] W. C. Lo, C. C. Yang, S. Y. Hsu, C. H. Chen, C. L. Yeh, and M. Hilpert,“The dynamic response of the water retention curve in unsaturated soils during drainage to acoustic excita-tions,” Water Resources Research, vol. 53, no. 1, pp. 712–725, 2017.
[18] D. M. O'Carroll, T. J. Phelan, and L. M. Abriola,“Exploring dynamic effects in capillary pressure in multistep outflow experiments,” Water Resources Research, vol. 41, no. 11, 2005. [19] T. Sakaki, D. M. O'Carroll, and T. H. Illangasekare, “Direct quantification of dynamic effects in capillary pressure for drainage-wetting cycles,” Vadose Zone Journal, vol. 9, no. 2, 2010.
[20] F. Stauffer, “Time dependence of the relations between capil-lary pressure, water content and conductivity during drainage of porous media,” in IAHR Symp. on Scale Effects in Porous Media. Thessaloniki Greece 29 Aug.-1. IAHR, Madrid, Spain, 1978.
[21] L. Zhuang, S. M. Hassanizadeh, C. Z. Qin, and A. de Waal, “Experimental investigation of hysteretic dynamic capillarity effect in unsaturated flow,” Water Resources Research, vol. 53, no. 11, pp. 9078–9088, 2017.
[22] S. M. Hassanizadeh and W. G. Gray,“Mechanics and thermo-dynamics of multiphaseflow in porous media including inter-phase boundaries,” Advances in Water Resources, vol. 13, no. 4, pp. 169–186, 1990.
[23] T. Annaka and S. Hanayama,“Dynamic water-entry pressure for initially dry glass beads and sea sand,” Vadose Zone Jour-nal, vol. 4, no. 1, pp. 127–133, 2005.
[24] D. A. DiCarlo,“Stability of gravity-driven multiphase flow in porous media: 40 years of advancements,” Water Resources Research, vol. 49, no. 8, pp. 4531–4544, 2013.
[25] S. L. Geiger and D. S. Durnford,“Infiltration in homogeneous sands and a mechanistic model of unstableflow,” Soil Science Society of America Journal, vol. 64, no. 2, 2000.
[26] E. Pellichero, R. Glantz, M. Burns, D. Mallick, S. Y. Hsu, and M. Hilpert, “Dynamic capillary pressure during water infil-tration: experiments and Green-Ampt modeling,” Water Resources Research, vol. 48, no. 6, 2012.
[27] N. Weisbrod, T. McGinnis, M. L. Rockhold, M. R. Niemet, and J. S. Selker,“Effective Darcy-scale contact angles in porous media imbibing solutions of various surface tensions,” Water Resources Research, vol. 45, no. 4, 2009.
[28] D. A. Weitz, J. P. Stokes, R. C. Ball, and A. P. Kushnick, “Dynamic capillary pressure in porous media: origin of the viscous-fingering length scale,” Physical Review Letters, vol. 59, no. 26, pp. 2967–2970, 1987.
[29] S. Y. Hsu and M. Hilpert,“Incorporation of dynamic capillary pressure into the Green-Ampt model for infiltration,” Vadose Zone Journal, vol. 10, no. 2, 2011.
[30] T. Tabuchi,“Infiltration and capillarity in the particle pack-ing,” Records Land Reclam Res., vol. 19, pp. 1–121, 1971. [31] P. G. D. Gennes, X. Hua, and P. Levinson,“Dynamics of
wet-ting: local contact angles,” Journal of Fluid Mechanics, vol. 212, no. 1, p. 55, 1990.
[32] P. Joos, P. van Remoortere, and M. Bracke,“The kinetics of wetting in a capillary,” Journal of Colloid and Interface Science, vol. 136, no. 1, pp. 189–197, 1990.
[33] T. E. Mumley, C. J. Radke, and M. C. Williams,“Kinetics of liquid/liquid capillary rise,” Journal of Colloid and Interface Science, vol. 109, no. 2, pp. 398–412, 1986.
[34] E. Schäffer and P.-z. Wong, “Contact line dynamics near the pinning threshold: a capillary rise and fall experiment,” Physi-cal Review E, vol. 61, no. 5, pp. 5257–5277, 2000.
[35] G. Camps-Roach, D. M. O'Carroll, T. A. Newson, T. Sakaki, and T. H. Illangasekare, “Experimental investigation of dynamic effects in capillary pressure: grain size dependency and upscaling,” Water Resources Research, vol. 46, no. 8, 2010. [36] D. A. DiCarlo, “Experimental measurements of saturation overshoot on infiltration,” Water Resources Research, vol. 40, no. 4, 2004.
[37] D. Wildenschild, J. W. Hopmans, and J. Simunek,“Flow rate dependence of soil hydraulic characteristics,” Soil Science Soci-ety of America Journal, vol. 65, no. 1, 2001.
[38] M. Hilpert, “Velocity-dependent capillary pressure in theory for variably-saturated liquid infiltration into porous media,” Geophysical Research Letters, vol. 39, no. 6, 2012.
[39] Z. Wang, J. Feyen, and D. E. Elrick,“Prediction of fingering in porous media,” Water Resources Research, vol. 34, no. 9, pp. 2183–2190, 1998.
[40] R. J. Glass, J. Y. Parlange, and T. S. Steenhuis,“Immiscible dis-placement in porous media: stability analysis of three-dimen-sional, axisymmetric disturbances with application to gravity-driven wetting front instability,” Water Resources Research, vol. 27, no. 8, pp. 1947–1956, 1991.
[41] M. D. Fredlund, D. G. Fredlund, and G. W. Wilson,“An equa-tion to represent grain-size distribuequa-tion,” Canadian Geotechni-cal Journal, vol. 37, no. 4, pp. 817–827, 2000.
[42] G. A. F. Seber and C. J. Wild, Nonlinear Regression, Wiley-Interscience, Hoboken, N.J, 2003.
[43] S. P. Friedman,“Dynamic contact angle explanation of flow rate-dependent saturation-pressure relationships during tran-sient liquid flow in unsaturated porous media,” Journal of Adhesion Science and Technology, vol. 13, no. 12, pp. 1495– 1518, 1999.
[44] P. W. Glover and E. Walker,“Grain-size to effective pore-size transformation derived from electrokinetic theory,” Geophys-ics, vol. 74, no. 1, pp. E17–E29, 2009.
[45] L. Makkonen, “A thermodynamic model of contact angle hysteresis,” The Journal of Chemical Physics, vol. 147, no. 6, article 64703, 2017.
[46] L. H. Tanner,“The spreading of silicone oil drops on horizon-tal surfaces,” Journal of Physics D, vol. 12, no. 9, pp. 1473– 1484, 1979.
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