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7/27/2019 Modeling of hydrogen-rich gas production by plasma reforming of hydrocarbon fuels.pdf
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International Journal of Hydrogen Energy 31 (2006) 769–774
www.elsevier.com/locate/ijhydene
Modeling of hydrogen-rich gas production by plasma reforming of hydrocarbon fuels
M.S. Benilova,∗, G.V. Naidisb
a Departamento de Física, Universidade da Madeira, Largo do Municipio, 9000 Funchal, Portugalb Institute for High Temperatures, Russian Academy of Sciences, Moscow 125412, Russia
Available online 9 August 2005
Abstract
The work is devoted to simulation of plasma reforming of hydrocarbon gases by means of a kinetic approach. It is shown
that the use of standard kinetic schemes, without inclusion of specific plasma processes, is sufficient for simulation of hydrogen
production in discharges with hot plasmas, in particular, in low-current arc discharges. Results of simulation of methane
and octane reforming are compared with data of experiments with low-current arcs available in the literature. An amount of
hydrogen produced in octane reforming is calculated for a wide range of mixture compositions, temperatures at the reactor
entrance, and discharge powers.
᭧ 2005 International Association for Hydrogen Energy. Published by Elsevier Ltd. All rights reserved.
1. Introduction
Plasma-chemical methods of hydrogen production from
natural gas and liquid hydrocarbon fuels through partial oxi-
dation and steam reforming processes are considered among
the most promising. Recently, a number of works have ap-
peared on the experimental study of plasma reforming of
mixtures of hydrocarbons with air and steam by means of
gas discharges of various types [1–9]. Typically, the effi-
ciency of hydrogen production with the use of cold plas-
mas, at gas temperatures in the discharge being lower than
400–500K (dielectric barrier discharges, coronas), is rela-
tively low: the values of QH2 , the discharge energy requiredfor production of one gram of H2, exceed 30 kJ/g (or 0.6 eV
per one H2 molecule). Higher efficiency has been reached
with the use of arc discharges at low currents (of the order
of 10−2–10−1 A) and near atmospheric pressures [6,7]. In
particular, values of QH2 in the range 3–13kJ/g were ob-
tained in partial oxidation of diesel fuel [6]. Note that though
the plasma state in low-current arcs (at discharge currents
∗ Corresponding author. Fax: +391 291 705269.
E-mail address: [email protected] (M.S. Benilov).
0360-3199/$30.00 ᭧ 2005 International Association for Hydrogen Energy. Published by Elsevier Ltd. All rights reserved.
doi:10.1016/j.ijhydene.2005.06.018
about several tens of milliamperes) in molecular gases atatmospheric pressure may deviate from equilibrium, the gas
temperature T c in the arc core is relatively high. For example,
values of T c in atmospheric-pressure arcs in air at currents
in the range 10−2–10−1 A are about 2000–3000 K [10].
Similar T c values have been obtained for this current range
also in our calculations of arc discharges in mixtures of air
with hydrocarbons [11].
The effect of plasma may consist both in gas heating
and in generation of chemically active species (excited
molecules, radicals, ions, electrons) in collisions of gas
molecules with electrons. The latter process is, evidently,
dominating in cold plasmas, where the gas heating is small.Both experiments and calculations show that the energy
cost of active species in discharges with cold plasmas is
usually rather high, about several electron Volts [12]. The
energy cost of active species in discharges with hot plas-
mas (arcs) is even higher than that in discharges with cold
plasmas, because in arc discharges a major part of the
energy input goes to gas heating. Therefore, the plasma
processing of hydrocarbon gases due to production of ac-
tive species could be energetically effective only in the case
if these active species are capable of participating in chain
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770 M.S. Benilov, G.V. Naidis / International Journal of Hydrogen Energy 31 (2006) 769– 774
reactions, that is, to serve as catalysts. (Note that possi-
ble mechanisms of plasma catalysis of hydrocarbons due
to ion–molecule reactions are discussed in [13,14].) Ac-
cording to the experimental data cited above, discharges
with cold plasmas (dielectric barrier discharges, coronas),
where the discharge effect is mainly in generation of active
species, produce hydrogen less efficiently than those with
hot plasmas (arc discharges). Therefore, one may assume
that for hot plasmas the effect of gas heating plays the major
role.
In [15,16] an analysis of the reforming process, aimed
at the search of optimal conditions for hydrogen produc-
tion, has been performed on the basis of thermodynamic ap-
proach. However, in general such approach is insufficient:
the effective time of the overall chemical process should
not exceed the residence time of reacting mixture inside the
chemical reactor, the latter being typically in the range of
seconds. Thus, more realistic estimates of parameters of the
reforming process are required. Such estimates can be ob-tained using a kinetic approach.
In this work, the known kinetic schemes for oxidation of
hydrocarbon gases are used for simulation of methane and
octane reforming in discharges with hot plasmas. On the ba-
sis of above considerations, the effect on hydrogen produc-
tion of active species generated by discharges is assumed
to be much smaller than that of gas heating. Therefore, no
discharge-related non-equilibrium reactions are taken into
account. The conditions are considered close to those real-
ising in experiments with low-current arcs.
2. The model
To simulate the plasma reforming process, a simple ap-
proach is used in which the discharge is accounted for as
an additional, with respect to chemical processes, energy
source inside the reactor. Calculations of chemical transfor-
mations, based on assumption of a perfect mixing of species
inside the reactor chamber, are performed using the code
PSR from the CHEMKIN-II package [17]. Input parame-
ters for the code are the gas composition and temperature
T ent at the reactor entrance, pressure p, the reactor volume
V , the total mass flow rate G and the power loss from the
reactor W loss. To account for the energy input from the dis-charge, the value of W loss in our calculations is taken nega-
tive, W loss =−W , where W is the discharge power. Output
parameters are the gas composition at the reactor exit and
the temperature inside the reactor.
Partial oxidation of two hydrocarbon fuels has been sim-
ulated, methane and octane (the latter is conventionally con-
sidered as a substitute of gasoline, e.g., [1]), in empty reac-
tors in the absence of catalysts inside the reactor chamber.
Kinetic schemes of reforming are based on mechanisms of
fuel oxidation available in the literature. For simulation of
methane reforming, two kinetic schemes have been used:
GRI-Mech 3.0 [18] and the Leeds methane oxidation mech-
anism version 1.5 [19]. Simulation of octane reforming has
been performed using the kinetic scheme [20].
Composition of the mixture of hydrocarbon CnHm with
air and steam at the reactor entrance is characterized by
two parameters, O/C ratio, defined as 2[O2]/n[CnHm],
and H2O/C ratio, defined as [H2O]/n[CnHm]. Here [O2],
[H2O] and [CnHm] are the volume flow rates of oxygen,
water and hydrocarbon.
3. Results of simulation
3.1. Methane reforming
Plasma reforming of methane–air mixtures has been sim-
ulated for conditions close to those of experiment [6]. The
results of simulation are given in Figs. 1 and 2. O/C ratio
was varied from 0.4 to 0.8, H2O/C ratio was taken equal to
zero. Fig. 1 shows the ratio H2/CO of the molar fractionsof H2 and CO in the reforming products versus O/C ratio;
two lines correspond to the results obtained using two above
mentioned mechanisms of methane combustion [18,19]. In
the same figure experimental data are shown, for two O/C
ratios ([6], Table 10, variants 3 and 4). It is seen that both
kinetic schemes give the values of H2/CO ratio rather close
to those measured. However, the results obtained with the
Leeds scheme [19] are in a better agreement with the ex-
periment concerning the trend of variation of H2/CO ratio
with the change of O/C.
Fig. 1. The ratio of the molar fractions of H2 and CO at methane
reforming versus O/C ratio at p=1bar, V =10−3 m3, W =1kW,
T ent = 300 K, the ratio of the discharge power to the total
volume flow rate 0.59kWh/m3(n). Lines—simulation, points—
experiment [6].
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Fig. 2. The ratio of the discharge power to the sum of volume
flow rates of produced H2 and CO at methane reforming versus
O/C ratio at conditions the same as in Fig. 1. Lines—simulation,
points—experiment [6].
In Fig. 2 the parameter SER, defined in [6] as the ra-
tio of the discharge power to the sum of volume flow rates
of H2 and CO produced, is shown versus O/C ratio. Both
schemes give the values of SER somewhat lower than those
measured. That is, the calculated efficiency of syngas pro-duction is higher than that obtained experimentally. Possi-
bly, this discrepancy occurs because the calculation does not
account for the thermal losses that are inevitably present in
experiment.
Note that the calculated gas temperature inside the re-
actor is rather high under the conditions considered above,
in the range 1400–1600 K. Such strong gas heating at rela-
tively small O/C ratios is mainly due to the energy supplied
by the discharge. At low energy inputs from the discharge,
when the gas heating is mainly due to the energy released at
methane oxidation process, considerably larger O/C ratios
should be employed. In [15], on the basis of the thermo-
dynamic analysis, it has been shown that optimal hydrogenyields correspond to the ratios of molar fractions of air and
methane in the range 3–3.5, that is, to O/C ratios in the range
1.3–1.5. The adiabatic gas temperature, calculated using the
relation of equality of the total enthalpies of reactants and
products, in these conditions is lower than 1200 K. (Note
that the adiabatic gas temperature is an increasing function
of O/C ratio.) The kinetic analysis shows that at such low
temperatures the time of establishment of equilibrium in an
empty reactor (without catalysts) is very large. As an exam-
ple, in Fig. 3 the results are given for simulation of chemical
transformations for O/C = 1.6, p = 1 bar at constant time
temperature 1270 K (the equilibrium adiabatic temperature).
Fig. 3. The molar fractions of H2, CO, CO2 and CH4 versus the
time of methane reforming at O/C = 1.6, p = 1bar, T = 1270 K.
Calculations have been performed using the code SENKIN
from the CHEMKIN-II package and the Leeds scheme of
methane oxidation. The molar fractions of various compo-
nents are shown as functions of time elapsed since the be-
ginning of chemical processes. It is seen that formation of
final products, H2 and CO, is a result of a complex chain of
chemical transformations, with a wide spectrum of reaction
times. At the first, fast stage of the reforming, at t < 0.1 s,
there is a steep decrease of XCH4 and a steep increase of
XH2 . However, at this stage only about one-third of hydro-
gen molecules are formed. Most of hydrogen is produced at
the second stage, which takes much more time. Therefore,
in order to provide fast enough methane reforming in the
absence of catalysts and at a relatively small energy input
from the discharge, O/C ratios should be taken substantially
larger than those corresponding to optimal hydrogen yields
estimated using thermodynamic approach.
3.2. Octane reforming
In Fig. 4 the composition of products of octane reforming
is given versus O/C ratio, simulated for conditions close
to those of experiment [7]; H2O/C ratio is taken equal to
zero. In the same figure, the molar fractions of products
are presented, measured in [7] at O/C = 1.32. It is seen
that the calculated composition of products is consistent
with that obtained in the experiment. Calculated temperature
inside the reactor increases with O/C ratio from 1300 K
(at O/C = 0.8) to 1600K (at O/C = 1.32) to 1900 K (at
O/C = 1.8).
Carbon monoxide obtained at partial oxidation of a hy-
drocarbon fuel may produce hydrogen in water shift reaction
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772 M.S. Benilov, G.V. Naidis / International Journal of Hydrogen Energy 31 (2006) 769– 774
Fig. 4. The molar fractions of products (in %) of octane re-
forming versus O/C ratio at p = 1bar, V = 2 × 10−3 m3,
W = 0.27kW, T ent = 300K, Gfuel = 0.26 g/s. Lines—simulation;
points—experiment [7]: — H2, — CO, ♦ — CO2, — CH4.
CO+H2O → CO2 +H2. (Note that the equilibrium in this
process is shifted to the right-hand side only at rather low
temperatures, T < 800 K. As partial oxidation proceeds fast
enough in the absence of catalysts at much higher tempera-
tures, the water shift can proceed only after cooling of par-tial oxidation products. At the stage of water shift, the use
of a catalyst is required because the time of overall process
in the gas phase at T < 800 K is unreasonably large.) One
of the parameters characterizing the efficiency of reforming
process is the ratio GH2/Gfuel of the mass flow rate of pro-
duced hydrogen, potentially accessible after water shift, to
the mass flow rate of fuel. In Fig. 5 the ratio GH2/Gfuel
is given versus O/C ratio, calculated for octane–air mixture
(without water) for various values of T ent and W . Optimal
O/C ratios, resulting in the highest hydrogen yield, are in
the range 1.3–1.5, corresponding to the ratio of air and fuel
mass flow rates at the reactor entrance Gair/Gfuel = 6–7.
It is seen that preheating of air–fuel mixture leads to a no-ticeable increase of hydrogen yield. The effect of discharge
power is relatively weak due to smallness of the energy in-
put provided by the discharge in comparison with the chem-
ical energy released in partial oxidation process. The role of
the discharge in these conditions is, evidently, mainly in the
formation of high-temperature regions where an ignition of
the reacting mixture occurs.
At small values of H2O/C ratio, the molar fraction of
H2O in the products of partial oxidation is smaller than that
of CO. In this case an additional amount of water should be
injected before the water shift stage. The effect of addition of
water to fuel–air mixture at the reactor entrance is illustrated
Fig. 5. The ratio GH2/Gfuel at octane reforming versus O/C ratio
at p = 2bar, V = 3× 10−3 m3, Gfuel = 1 g/s.
Fig. 6. The molar fractions of products (in %) of octane reforming
versus H2O/C ratio at O/C = 1.4, V = 3× 10−3 m3, p = 2bar,
T ent = 800K, W = 0.3kW, Gfuel = 1 g/s.
by Fig. 6, where the calculated composition of products is
given versus H2O/C ratio. Increase of H2O/C ratio results
in decrease of the molar fraction of CO and increase of that
of H2O. Fig. 6 shows that the use of mixtures with H2O/C
ratio about 0.5 (corresponding to the ratio of water and fuel
mass flow rates at the reactor entrance GH2O/Gfuel about
0.6) allows one to get, after partial oxidation, the mixture
with nearly equal molar fractions of H2O and CO. Note
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Fig. 7. The ratio GH2/Gfuel at octane reforming versus the dis-
charge power at O/C = 1.4, p = 2bar, V = 3× 10−3 m3.
that the effect of H2O/C ratio on hydrogen yield is not
substantial. It follows that the amount of water required for
water shift process may be added to the fuel–air mixture not
necessarily after fuel reforming in partial oxidation process,
but already at the first stage, before reforming.
The effect of discharge power on hydrogen yield is shown
in Fig. 7 where the ratio GH2
/Gfuel, potentially accessible
after water shift, is given versus W , for various values of T ent
and H2O/C ratio. It is seen that increase of W by about an
order of magnitude results in an increase of GH2 not exceed-
ing 10%. Such weak effect of W is due to smallness of the
energy input provided by the discharge in comparison with
the chemical energy released in partial oxidation process.
4. Conclusions
A kinetic approach to analysis of plasma reforming of
hydrocarbon gases based on the use of standard kinetic
schemes available in the literature without any additionaladjustments gives results which are in a reasonable agree-
ment with experimental data on low-current arc discharges.
This approach allows one to specify optimal conditions for
reforming process. In particular, for partial oxidation of oc-
tane in empty reactor (without a catalyst) the initial mix-
ture composition with O/C ratio about 1.3–1.5 is prefer-
able. Two stages of reforming, partial oxidation (stage 1)
and water shift (stage 2) should proceed separately. Before
the second stage, the mixture is to be cooled to temperatures
lower than 800 K. For water shift the use of a catalyst (e.g.,
based on iron oxide) is required. Cooling of the products of
partial oxidation before water shift stage may be provided
by means of heat exchange with the species before they en-
ter the reactor. Such heat exchange would also preheat the
mixture, thus enhancing hydrogen yield at the first stage of
reforming.
A use of regimes with high O/C ratios, where the re-
quired energy is provided by exothermic chemical reactions
of oxidation of fuel, allows one to work at relatively low
discharge powers. In these regimes the role of discharge
is mainly in mixture ignition, like in spark-ignited gaso-
line engines. Some threshold value of the discharge power
must exist that is required to ensure ignition. An extrapola-
tion of experimental data [7] gives, for the fuel mass flow
rate 1 g/s, the discharge power, sufficient for ignition, about
1 kW. Corresponding value of the energy consumption for
hydrogen production is about 5 kJ/g (about 0.1 eV per one
H2 molecule).
Acknowledgements
The work was supported by the EC through the project
No. ENK5-CT-2000-00346.
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