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ANLISIS DE SENSIBILIDAD EN UN REACTOR DE CRAQUEO CATALTI-CO DE METANO PARA LA PRODUCCIN DE HIDRGENO
J. Pulgarn-Len1, J. Saavedra-Rueda2, A. Molina1,*1 Bioprocesos y Flujos Reactivos, Facultad de Minas, Universidad Nacional de Colombia, Sede Medelln
2 Instituto Colombiano del Petrleo, Ecopetrol, Bucaramanga
Resumen:Se desarroll un modelo de un reactor de craqueo cataltico de metanopara la produccin de hidrgeno utilizando un mecanismo que simplifica las
mltiples reacciones heterogneas que suceden en el reformado cataltico con tresreacciones que incluyen la adsorcin en sitios activos y el equilibrio qumico. El
modelo considera al reactor como un lecho empacado y simplifica la transferencia
de masa en el catalizador considerando las reacciones como pseudohomogneas.
Para el desarrollo del modelo se utiliz el software comercial ASPEN Plus y se es-
cribi un mdulo de usuario que utiliza una rutina en FORTRAN escrita especfi-camente para representar la cintica qumica. Las predicciones del modelo son si-
milares a las tendencias reportadas en la literatura y en un reformador industrial. El
artculo concluye utilizando el modelo para entender el efecto de la variacin de latemperatura, relacin vapor/carbono y tiempo de residencia sobre la conversin y
el rendimiento fraccional global para el hidrgeno.
Palabras Clave:Reformado de metano, Gas natural, Hidrgeno, ASPEN PLUS.
SENSITIVITY ANALYSIS OF A METHANE STEAM REFORMER
J. Pulgarn-Len1, J. Saavedra-Rueda2, A. Molina1,*1 Bioprocesos y Flujos Reactivos, Facultad de Minas, Universidad Nacional de Colombia, Sede Medelln
2 Instituto Colombiano del Petrleo, Ecopetrol, Bucaramanga
Abstract:A model that predicts the conversion in a methane steam reformer for
hydrogen production was developed. The model makes use of a three-reactionmechanism that simplifies the multiple heterogeneous reactions involved in re-
forming that include adsorption on catalyst active sites and chemical equilibrium.
The model considers the reformer as a packed bed and simplifies mass transfer in
the catalyst by considering reactions as pseudohomogeneous. The model was de-
veloped using a FORTRAN subroutine specially written for the former that waslinked to the commercial software ASPEN Plus. Model predictions are similar to
those found in the literature and with results from an industrial reformer. The pa-
per ends with a sensitivity analysis that uses the model to understand the effect that
the variation of temperature, steam to carbon ratio and residence time have on me-
thane conversion and on fractional conversion of hydrogen.
Keywords:Methane steam reforming, Natural Gas, Hydrogen, ASPEN PLUS.
*Corresponding author: [email protected]
1. IntroductionDespite the recent interest in different
technologies for hydrogen production,
such as biomass and coal gasification,
fluidized bed membrane reactors, fermen-
tative routes and water electrolysis; me-
thane steam reforming remains the major
production route of hydrogen. Although
this interest is mainly motivated by the
role that hydrogen can play as an energy
resource, hydrogen production for the
petrochemical, chemical and food industry
will remain a major activity of chemical
engineers.
In methane steam reforming, hydrogen is
produced in a furnace in which a mixture
of methane and water reacts in tubes iso-
lated from the combustion gases. With thehelp of a catalyst (typically with Ni as
major component) a highly endothermic
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2
reaction converts methane and water into
a mixture of hydrogen and other com-
pounds, with carbon monoxide as major
component.
There is a vast literature on modeling
steam reformers. [1-22]. Most studies
date to the late 80s. In the 90s and early
21st century the number of papers in the
open literature on modeling methane
steam reformers decreased, probably be-
cause of licensing agreements between
production companies and research insti-
tutions as well as an increased interest in
alternative technologies for reforming
such as Fluidized Bed Membrane Reac-tors [10, 13, 16-19], optimized control
strategies [12, 14, 15] and novel catalysts
formulations [11, 21].
One of the most refereed studies on me-
thane reformers was the work by Xu and
Froment [5, 7] that describes a model for
these reactors and carefully compares
experimental data with predictions. In
Colombia, as early as in 1981, Ros de-
veloped a model that predicted hydrogen
production and methane conversion in anindustrial methane steam reformer [1].
More recently Acua [14], in order to
improve the controllability of steam re-
formers, developed a detailed model of
the methane steam reforming process.
This paper presents preliminary results on
a model that predicts the conversion of
steam and methane in a reformer. Model
details, such as kinetic expressions and
input parameters are defined. The resultsfrom the model are validated against pre-
vious literature results, and data from an
industrial reformer. The paper ends with a
sensitivity analysis that allows an addi-
tional test to the model and further under-
standing of the methane steam reforming
reaction. The results show that the model
can correctly predict most of the trends
observed in an industrial reformer.
2. ModelTo simulate the conversion of methane to
hydrogen in a catalytic reactor it is neces-
sary to consider three elements: (1) the
kinetic expressions that describe the rateof methane and water reaction on the cata-
lyst surface to produce hydrogen and other
byproducts, (2) the mathematical expres-
sions that address the mole, momentum
and energy balances in the reactor and (3)
the process parameters (both operational
and geometrical) that characterize the
reactor.
2.1 Kinetic data
As mentioned in the introduction, bothRos [1] and Acua [14] modeled methane
steam reformers. While Ros fitted expe-
rimental data to obtain the kinetic parame-
ters for his model, Acua [14] used the
kinetic expressions described by Haldor
[23], as quoted by Acua [14], that date
from 1965. The present research aimed at
making use of more contemporary kinetic
data.
A review of previous literature showed
that the model proposed by Xu and Fro-ment [7] in 1989 is the one more quoted in
the literature. Although it is an old model,
it was recently successfully used by Za-
maniyan et al. [20] and Alberton et al.
[22] in the simulation of industrial me-
thane reformers.
Table 1shows the reactions considered by
Xu and Fromment [7].
These authors came to the conclusion that
reactions R 6 to R 11 are not important
because the ratios of forward to reverse
reaction rates are always higher than 1 at
typical steam reforming conditions. Reac-
tions R 4 to R 5 are also considered of
minor importance because they, although
thermodynamically favored at typical
reforming conditions, describe trends
(lower CO2concentration as the length in
the reactor increases) that do not agree
with normal reactor performance. Al-
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3
though these are rather weak assumptions
as local conditions inside the reformer
may have concentrations that will thermo-
dynamically favor forward reactions, as a
first approximation in this paper, we
adopted Xu and Fromment [7] recom-
mendations and simply considered R 1 to
R 3 as the most important reactions in the
process.
Table 1. Reactions involved in methane steam reforming as reportedby Xu and Fromment [7]
Reaction H298(kJ/mol)
R 1224 H3COOHCH 206.1
R 2222 HCOOHCO 41.15
R 3224 H4COOH2CH 165.0
R 4224 H2CO2COCH 247.3
R 5 OH2CO4CO3CH 224
330.0R 6
24 H2CCH 74.82R 7
2COCCO2 173.3
R 8 OHCHCO 22 131.3R 9 OH2CH2CO 222 90.13
R 10 OH2C3CO2CH 24 187.6R 11 OH2C2COCH 224 15.3
Xu and Fromment [7] carried out a bal-
ance of active sites on the catalysts for aheterogeneous mechanisms they devel-
oped to simulate R 1 to R 3. From this
balance these authors derived three rate
expressions shown in E 1 toE 3 that con-
sider the partial pressure of hydrogen,
methane, water and carbon monoxide, (Pi)
as well as kinetic (ki), equilibrium (Ki) and
adsorption constants (Kj, with j represents
CO, H2, CH4, H2O). E 5 toE 7present the
mathematical expressions used to
represent the variation of the constant withtemperature. Table 2 to Table 4 show the
kinetic constants finally used in the model.
Equilibrium constants were calculated
using the free-domain code for gaseous
equilibrium Gas-Eq [24].
2
1
CO
3
OHCH5.2
2H
1
1DEN
K
pppp
p
k3
r
2H
24
E 1
2
2
COH
OHCO2H
2
2DEN
K
pp
ppp
k
r
22
2
E 2
2
3
CO
4
4
4CH5.3
2H
3
3DEN
K
pppp
p
k4
r
22H
O2H
E 3
2
2
244
22
H
OH
OHCHCH
HHCOCO
p
pKpK
pKpK1
DEN E 4
ir
T,iiT
1
T
1
R
Eaexpkk
E 5
ir
j
T,iiT
1
T
1
R
HexpKK
E 6
i
ibi
ii,eqT
EaexpTAK
E 7
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Table 2. Kinetic constants used in the model(adapted from [7])
ki, 648K Eai
(kmol bar1/2
/ kg cat h) (kJ/mol)
k1 1.84 10-4 240.1
k2 7.558 67.13
k3 2.19 10-5
243.9
Table 3. Adsorption constants used in the model(adapted from [7])
Kj TrH
(bar-1
) (K) (kJ/mol)
CH4 0.1791 823 -38.28
H2O 0.4152* 823 88.68CO 40.91 648 -70.65
H2 0.02960 648 -82.90
*Dimensionless
Table 4. Equilibrium constants used in the mod-el (calculated from[24])
Ai (bar2) bi Eai (K
-1)
Keq1 4.94106 1.89 -25216
Keq2 1.2010-6
* 1.24 5425
Keq3 5.93 3.13 -19791
*Dimensionless
2.2 Balance equations in the reactorAs one of the objectives of the paper was
to perform a sensitivity analysis of the
methane steam reformer and given the
extended use of the commercial software
ASPEN in the Chemical Engineering in-
dustry, this research employed ASPEN
PLUS V 7.0, as simulation tool. Unfortu-
nately, as it happens with most commer-
cial software, the presence of non-conventional kinetic expressions, (e.g.E 1
to E 3), impose the use of user-defined
models in ASPEN.
There are typically two possibilities when
modeling non-conventional rate expres-
sions in ASPEN. The first one, as illu-
strated by Barrera et al. [25], consists in
linking ASPEN to Excel and developing
the kinetic expressions through Excel by a
spreadsheet. The second one, adopted in
this research, consist on defining FOR-
TRAN-based subroutines. We consider the
second approach more suited for our re-
search needs as FORTRAN allows more
complex calculations that Excel.
As this was the first time that FORTRAN
was linked with ASPEN in our research
group, we developed our own code to
model a PFR reactor using MATLAB to
validate the ASPEN/FORTRAN approach.
Both programs (MATLAB and AS-
PEN/FORTRAN) yielded identical results.
Although the methane steam reformer
simulations by Ros [1] and Acua [14]
considered energy and momentum bal-ances inside the reactor, this research used
predefined pressure and temperature pro-
files as inputs to the model. This was done
because emphasis was placed in the kinet-
ic approach and, as a first step; it was con-
sidered more important to address the
chemistry. Current work conducted in our
research group, is incorporating energy
and momentum expressions to the model.
In the treatment of the reactor in ASPENwe adopted a PFR formulation and consi-
dered did not consider heterogeneous limi-
tations (pseudo-homogeneous approach).
This is clearly an oversimplification, al-
though frequently adopted in the literature
(e.g. [1, 14]). Future developments of the
FORTRAN subroutine will include mass
transfer to the particle with approaches
similar to those described by Xu and
Fromment [5], Zamaniyan et al. [20] and
Alberton et al. [22]
2.3 Process and reactor parametersAlthough, as explained above, the AS-
PEN/FORTRAN reactor model was vali-
dated with an independent program de-
signed by our research group, additional
validation of the kinetic expressions was
mandatory before simulation of an indus-
trial furnace could be undertaken. This
kinetic validation was carried out using the
data presented by Zamaniyan et al. [20]. A
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5
comparison of our results with those of
Zamaniyan et al. [20] is presented in the
Results section.
In the simulations used to validate our
model against that of Zamaniyan et al.
[20], we employed the same input parame-
ters (temperature and pressure profile,
geometry, input stream gas composition,
temperature and pressure profiles) that
Zamaniyan describe in their paper [20].
For the simulation of the industrial me-
thane steam reformer a 15-m length, 12.6-
cm internal diameter reactor was consi-
dered. Table 5 shows the input-stream
composition as supplied by the reformeroperator. O2 and N2 were considered as
inert gases, given their low concentrations.
The concentrations of ethane, propane and
butane were added to that of methane fol-
lowing the equal-carbon concept described
by Zamaniyan et al. [20].
Table 5. Input-stream composition
Species CH4 H2O O2 N2Molar
fraction0.1384 0.8424 0.0003 0.0017
Species C2H6 C3H8 C4H10Molar
fraction0.0143 0.0027 0.0002
As only input and output data were availa-
ble for temperature and pressure, the tem-
perature and pressure profiles reported for
an industrial methane steam reformer in
the literature [20] were adjusted to obtain
the same input and output values as those
reported by the reformer operator. Figure1 compares the temperature and pressure
profiles used in this paper for the industri-
al reformer with those of Zaminiyan et al.
[20]. It is evident that the use of these
profiles is a rather crude simplification.
Nevertheless, as it will be shown below, it
turned out to be an acceptable approxima-
tion.
Because, mass-transfer limitations were
not modeled, no data on the catalyst is
given different from the fact that it was a
Ni/Al2O3 catalyst and the density was as-
sumed to be 2355.5 kg m-3, as reported in
[20].
3.Results and discussion3.1 Model validationFigure 2 compares the profiles of major
species (CH4, H2O, H2and CO) along the
reactor predicted by Zamaniyan et al. [20]
with those obtained using our model. Al-
though there are some clear differences in
trends, exit concentrations are very similar
for all species. Particularly the two more
important species, H2and CH4, show simi-
lar concentrations at the reactor exit. This
gives confidence on the model ability tocorrectly predict the final result for the
reactor.
600
800
1000
1200
0 2 4 6 8 10 12 14distance along reactor (m)
T(K)
Zamaniyan et al.
this paper
a.
11
12
13
14
15
16
17
0 2 4 6 8 10 12 14distance along reactor (m)
P(bar)
Zamaniyan et al.
this paper
b.
Figure 1. Comparison of (a) temperature and(b) pressure profiles along the reactor. Datafrom Zamaniyan et al. [20] and this paper
Contrary to the relative success in predict-
ing the final concentrations,Figure 2 a. to
d. show that our model tends to overesti-
mate methane conversion. This is evident
in Figure 2 because the predictions by
Zamaniyan et al. [20], show that methane
concentration is always higher and hydro-
gen concentration lower than our model
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0.0
0.1
0.2
0.3
0 2 4 6 8 10 12
distance along reactor (m)
CH4
(molfraction)
a.
Zamaniyan et al.
this paper
0.2
0.3
0.4
0.5
0 2 4 6 8 10 12
distance along reactor (m)
H2O
(molfraction)
b.
Zamaniyan et al.
this paper
0.0
0.1
0.2
0.3
0 2 4 6 8 10 12
distance along reactor (m)
H
2(molfraction)
Zamaniyan et al.
this paper
c.
0.0
0.1
0.2
0.3
0 2 4 6 8 10 12
distance along reactor (m)
CO(molfraction)
d.
Zamaniyan et al.
this paper
Figure 2. Comparison of concentration profiles as predicted by the model described by Zamaniyan et al. [20] and by this paper. (a)CH4, (b), H2O, (c) H2and (d) CO.
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results, at short distances inside the reac-
tor. This result is not surprising as Zama-
niyan et al. [20] considered mass-transfer
limitations inside the catalyst (using an
effectiveness factor) and our model consi-dered a pseudo-homogeneous approach.
Neglecting mass transfer limitations caus-
es the observed overestimation of methane
conversion at short distances in the reac-
tor. As stated above, future model ver-
sions should consider mass transfer limita-
tion in the catalyst.
3.2 Simulation of industrial methanesteam reformer.
Once the model was validated againstliterature data, the ability of the model to
predict the behavior in an industrial re-
former was addressed. Table 6 compares
the exit concentrations (in mole fractions)
as reported by the reformer operator with
model predictions. Although there are
some differences, particularly in CO, the
agreement between predictions and the
data for the industrial reformer is deemed
as excellent, considering some of the
crude approximations taken with the pres-sure and temperature profiles.
Table 6. Comparison of exit concentrations(mole fraction) in an industrial reformer with
model predictions
Industrial
reformer
Model
CH4 0.0110 0.0145
H2O 0.4536 0.4878
H2 0.4121 0.3885
CO 0.0600 0.0419
CO2 0.0620 0.0657
N2 0.0013 0.0015
3.3 Sensitivity analysisTo make an additional validation of the
model and get a better understanding of
the reforming reaction, a sensitivity analy-
sis of the model response to variations in
temperature profile, steam-to-carbon ratio
in
CS (in molar units) and residence
time was carried out. There are different
variables that can be used to evaluate the
performance of a methane steam reformer
(e.g. mass flow hydrogen produced, con-
version of different species, rate of coke
deposition, rate of H2to CO at the reactor
exit). Among those and for clarity of thediscussion we selected only two: conver-
sion of methane 4CHX defined as theratio of methane moles converted in the
reactor to those entering the reformer and
the fractional conversion of hydrogen
42 CHH defined inE 8.
(moles)convertedCH
molesreactor
theleavingH
CHH
4
2
42
E 8
Figure 3 shows the variation of methane
conversion 4CHX and hydrogen fraction-al conversion 42 CHH with changes innominal reactor temperature. Because
there is a temperature profile, the abscissa
inFigure 3 represents a nominal tempera-
ture that reflects the mean temperature in
the profile.
As expected, inFigure 3 methane conver-
sion increases with temperature. However,
42 CHH decreases, with temperature,as thermodynamic restrictions on the for-
ward reaction in R 3 augment with tem-
perature. Figure 3 suggests that a temper-
ature of the order of 1100 K guarantees
acceptable methane conversion, while the
fractional hydrogen conversion remains at
an acceptable value of 2.8. It is important
to note that accordingR 1 toR 3,the max-
imum possible value of 42 CHH is 4.A value of 2.8, such as that obtainedaround 1100 K, seems a good compromise
between methane conversion and hydro-
gen production.
As Figure 4 shows, a higher value in the
steam to carbon ratio in
CS favors both,
methane conversion and fractional con-
version to hydrogen. This happens be-
cause a higher steam concentration favors
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8
equilibrium toward hydrogen production
in E 3. Favoring hydrogen production
increases as well methane conversion.
0.0
0.2
0.4
0.6
0.8
1.0
700 900 1100 1300
temperature (K)
XCH4
2.4
2.6
2.8
3.0
3.2
(H2/CH4)
Figure 3. Predicted variation of methane con-
version 4CHX and fractional conversion ofhydrogen 42 CHH with changes in no-minal reactor temperature
0.0
0.2
0.4
0.6
0.8
1.0
4 5 6 7 8(S/C)in(mol/mol)
XCH4
2.4
2.6
2.8
3.0
3.2
(H2/CH4)
Figure 4. Predicted variation of methane con-
version 4CHX and hydrogen fractional con-version 42 CHH with steam-to-carbonratio
inCS
Figure 4 suggests that the use of a higher
value of in
CS would be advisable, as
higher methane conversion and fractional
conversion of hydrogen are desirable out-
comes. However, as Figure 5 shows, the
total mass flow of hydrogen2H
m de-
creases as the steam to carbon ratio in-
creases. Therefore, a balance between a
reduction on hydrogen production and an
increase in methane conversion and frac-
tional conversion of hydrogen needs to be
performed during reactor design. A final
sensitivity analysis was conducted for
residence time (Figure 6). The model
predicts a reduction on methane conver-
sion and fractional selectivity of hydrogen
as the residence time in the reactor de-
creases. This is an expected result. How-
ever, Figure 6 gives very important infor-mation for model validation as shows that
for typical conditions (residence time of
0.11 s) methane conversion and the frac-
tional conversion of hydrogen present a
plateau that favors stable operation.
900
1000
1100
1200
1300
3.5 4.5 5.5 6.5 7.5(S/C)in(mol/mol)
h/
kg
m
2
H
Figure 5. Predicted variation of hydrogen mass
flow2H
m with changes in the steam-to-carbon
ratio in
CS
0.0
0.2
0.4
0.6
0.8
1.0
0.00 0.02 0.04 0.06 0.08 0.10 0.12
residence time (s)
XCH4
2.4
2.6
2.8
3.0
3.2
(H2/CH4)
Figure 6. Predicted variation of methane con-
version 4CHX and hydrogen fractional con-version 42 CHH with residence time in thereactor
4. ConclusionsA model that integrates complex chemical
kinetics into ASPEN using a FORTRAN
subroutine correctly predicts the behavior
of an industrial methane steam reformer.
The model, validated against literature and
industrial data, was used to conduct a sen-
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9
sitivity analysis of methane conversion
and fractional conversion to hydrogen
with temperature, steam to carbon ratio
and residence time. Although the higher
the temperature, the higher the methaneconversion, thermodynamic restrictions
decrease methane and steam conversion to
hydrogen as temperature increases. A
nominal temperature of 1100 K seems to
give a reasonable balance between me-
thane conversion and factional conversion
of hydrogen. Higher steam to carbon ratio
favors both methane conversion and fac-
tional conversion of hydrogen, however it
decreases the mass flow of hydrogen. It is
necessary to establish a balance on prod-uctivity and conversion to assure optimal
reformer behavior. The model gives in-
formation on the variation of methane
conversion and fractional conversion of
hydrogen with residence time. The results
suggest that for the industrial reformer
analyzed, a residence time close to 0.12 s
is optimal because it guarantees that varia-
tions in residence time do not have a ma-
jor impact in conversion.
Acknowledgment
We acknowledge Aspen Technology for
having granted special permission for the
use of the ASPEN. PLUS under the condi-
tion of the academic licensing agreement.
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