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Article Open Access February 24, 2022

Computational Fluid Dynamics Modeling of Thermally Integrated Microchannel Reforming Reactors for Hydrogen Production

Junjie Chen 1,*
1
Department of Energy and Power Engineering, School of Mechanical and Power Engineering, Henan Polytechnic University, 2000 Century Avenue, Jiaozuo, Henan, 454000, P.R. China
Publihed in: Online Journal of Engineering Sciences (Volume 1, Issue 1, 2022)
Page(s): 29-44
DOI: 10.31586/ojes.2022.228
Received
January 02, 2022
Revised
February 10, 2022
Accepted
February 23, 2022
Published
February 24, 2022
Keywords
Reactor design; Microstructured reactors; Steam reforming; Computational fluid dynamics; Transport phenomena; Hydrogen production
Creative Commons

This is an Open Access article, distributed under the terms of the Creative Commons Attribution 4.0 International License (http://creativecommons.org/licenses/by/4.0/), which permits unrestricted use, distribution and reproduction in any medium or format, provided the original work is properly cited.
Copyright: Copyright © The Author(s), 2022. Published by Scientific Publications

Abstract

Many attempts have been made to improve heat transfer for thermally integrated microchannel reforming reactors. However, the mechanisms for the effects of design factors on heat transfer characteristics are still not fully understood. This study relates to a thermochemical process for producing hydrogen by the catalytic endothermic reaction of methanol with steam in a thermally integrated microchannel reforming reactor. Computational fluid dynamics simulations are conducted to better understand the consumption, generation, and exchange of thermal energy between endothermic and exothermic processes in the reactor. The effects of wall heat conduction properties and channel dimensions on heat transfer characteristics and reactor performance are investigated. Thermodynamic analysis is performed based on specific enthalpy to better understand the evolution of thermal energy in the reactor. The results indicate that the thermal conductivity of the channel walls is fundamentally important. Materials with high thermal conductivity are preferred for the channel walls. Thermally conductive ceramics and metals are well-suited. Wall materials with poor heat conduction properties degrade the reactor performance. Reaction heat flux profiles are considerably affected by channel dimensions. The peak reaction heat flux increases with the channel dimensions while maintaining the flow rates. The change in specific enthalpy is positive for the exothermic reaction and negative for the endothermic reaction. The change in specific sensible enthalpy is always positive. Design recommendations are made to improve thermal performance for the reactor.

1. Introduction

The steam reforming of hydrocarbon or alcohol fuels has attracted increasing interest in the context of the production of hydrogen [1, 2]. Typically, a traditional steam reforming reactor system consist of a reformer, which contains an appropriate reforming catalyst to facilitate the endothermic reforming reaction and a large industrial furnace to provide the necessary thermal energy for the reaction [3, 4]. A hydrocarbon or alcohol fuel and steam are supplied to the reformer, and hydrogen must be separated from the undesired product, carbon monoxide. An industrial steam methane reforming reactor typically contains an array of long and narrow tubes [5, 6], which are usually made of refractory alloys. The interiors of the tubes constitute the reaction region and the tubes are packed with commercial porous pellets of material, which are impregnated with an appropriate reforming catalyst. The heated length of the tubes is typically between 6 and 12 meters and the diameter of the tubes varies between 9 and 16 cm. The tubes are situated within the combustion chamber of the furnace. With respect to steam methane reforming processes, flame temperatures as high as 1300° C are typically employed to ensure that the temperature of the reaction lies within a range of about 800 to 900 °C [7, 8]. The furnace operates at temperatures considerably higher than the temperatures required by the reaction, since the combustion gases must transfer the heat of reaction to the reforming gases through the reactor walls and to the commercial catalyst pellets in which the reaction occurs. High flame temperatures up to about 1300° C are required in order to ensure that the reforming catalyst operates at the desired temperatures. However, high flame temperatures will inevitably cause the formation of nitrogen oxide. Furnace designs vary, but the volume is necessarily large.

Unfortunately, such industrial steam reforming reactors cannot be scaled to smaller dimensions for a modular portable unit so as to provide a sufficient hydrogen-rich reformed gas for a chemical reaction process or a fuel cell. For example, portable fuel cell systems can be used for commercial, industrial and residential primary and backup power generation [9, 10]. Portable fuel cell systems are of particular interest in remote or inaccessible areas [11, 12] and in undeveloped countries, which lack technological capability, a power grid, and the funds for an extensive electricity distribution infrastructure. Fuel cell vehicles are another area of interest, particularly for mass transit vehicles and trucks and for hybrid vehicle power trains [13, 14]. High purity hydrogen in high-pressure tanks is presently not desirable for fuel cell vehicles due to the volume and safety constraints. Consequently, the optimum solution will be the use of liquid hydrocarbon fuels, such as heptane [15, 16] and liquefied natural gas [17, 18], or the use of volatile fuels, such as alcohols [19, 20] and motor grade kerosene [21] and gasoline [22], in order to feed an on-board reforming reactor and produce form a hydrogen-rich product gas, commonly referred to as reformate, as the feedstock for fuel cell vehicles.

To solve the problems outlined above, various plate-type reforming reactors have been developed. These reactors are compact in size. Even at low temperatures, catalytic combustion can be carried out in such reactors. An example of such plate-type reforming reactors has been developed by Koga et al. [23]. The reforming reactor has alternating flat gap spaces for a fuel-air mixture and a fuel-steam mixture. The reforming gap spaces are filled with a reforming catalyst, while the combustion gap spaces are filled with a combustion catalyst. The necessary heat for the endothermic steam reforming reaction is supplied through the exothermic catalytic combustion reaction, with temperatures substantially lower than 1300° C. A more compact example of the plate-type reforming reactor has been developed by Igarashi et al. [24]. A rectangular wall reactor has been design, which consists of alternating stages comprising a heated reformer area separated from a conductive heating area [25, 26]. Each stage comprises a plurality of plates. For example, each stage is formed from three plates, a center partition plate and a pair of spaced boundary plates. A catalyst is deposited by applying electroless plating on the plate surfaces of the reforming reactor. The compact reforming reactor can achieve higher conversions than traditional reactors due to increased surface area for heat transfer.

However, the above plate-type reforming reactors have not been widely used, and the difficulties of design are a primary concern. For the plate-type reforming reactor described above [23], the reforming and combustion catalysts used to fill the gaps between the channel plates are in the form of pellets or particles. The catalyst systems do not adhere to the channel walls. As a result, the heat released by the exothermic catalytic combustion reaction must be transferred to the gas phase before reaching the reforming catalyst. Thermal energy is therefore transferred ineffectively within such a reaction system. Additionally, the reaction volume of the reactors is usually large, since a gaseous stream transfers the heat of reaction. For the compact plate-type reforming reactor described above [24], the reforming catalyst is deposited onto the walls of the reforming channels. Consequently, the heat of reaction must be transferred via thermal conduction to the reforming catalyst through the thermally conductive walls of the reactor, and in the combustion channels heat transfer still takes place between the fluid phase and the solid phase.

Another thermally integrated tubular-type reforming reactor has been developed by Ioannides and Verykios [27]. The tubular reactor consists of an inner non-porous ceramic channel with a high thermal conductivity and an outer U-shaped ceramic channel, with a structure of an endocentric construction. Additionally, the inside and outside surfaces of the inner channel are coated with similar or different metal catalyst layers [27, 28]. A reactant mixture consisting of methane and oxygen is introduced into the inner channel. The reaction mixture passes into the inner channel, thereby carrying out a combustion reaction by utilizing a catalyst. The reaction mixture then passes out the inner channel and passes into an annulus space between the inner and outer channels in the reverse direction. In the annulus space, a reforming reaction takes place within the reforming catalyst layer. A large fraction of the heat released by the exothermic catalytic combustion reaction is transferred towards the outer reforming catalyst layer across the channel wall. The design makes the reforming reactor more compact. However, the design is usually employed on a laboratory scale.

Accordingly, further study is needed to take the inherent myriad advantages associated with the tubular reactor. Design methods must also be developed to address the issues associated with scale-up of such continuous flow reactors. Recently, a thermally integrated microchannel chemical reactor has been developed for simultaneously conducting exothermic and endothermic reactions [29, 30]. The reactor consists of two separate sets of flow channels in an alternating, layered arrangement [31, 32]. The reactor comprises an exothermic heat exchange layer and an endothermic process layer [33, 34]. The dividing walls of the reactor have the same or different catalysts on opposed surfaces, which are selected for a particular reaction occurring in the adjacent reaction region [35, 36]. The heat of an exothermic reaction is transferred from the exothermic reaction catalyst to the endothermic reaction catalyst, in which the heat serves as a heat source for the endothermic reaction. Multiple modular reactor units could be stacked to provide a reaction system of any desired throughput capacity and portability [37, 38]. Alternately, a microchannel reforming reaction system can be formed by stacking modular reactor units [39, 40]. Methods have also been suggested for the catalytic reforming of hydrocarbon fuels for the production of hydrogen or synthesis gas by utilizing such a reactor [41, 42]. There is a continuing effort to perform steam reforming reactions in thermally integrated microchannel chemical reactors [43, 44]. However, the mechanisms for the effects of design factors on heat transfer characteristics are still not fully understood.

This study relates to a thermochemical process for producing hydrogen by the catalytic endothermic reaction of methanol with steam in a thermally integrated microchannel reforming reactor. Computational fluid dynamics simulations are conducted to better understand the consumption, generation, and exchange of thermal energy between endothermic and exothermic processes in the reactor. The effects of wall heat conduction properties and channel dimensions on heat transport characteristics and reactor performance are investigated. The objective of this study is to gain insight into the fundamental characteristics of heat transfer in thermally integrated microchannel reforming reaction systems. Particular emphasis is placed on the dependence of heat transfer characteristics on wall heat conduction properties and channel dimensions in various situations, with an attempt to improve the distribution of thermal energy for use in microchannel reforming reaction systems.

2. Description of the model

2.1. Description of the reactor
Figure 1
Schematic illustration of the thermally integrated microchannel methanol reforming reactor used for hydrogen production. The channel walls are not depicted for clarity.

The present study relates to a thermally integrated microchannel methanol reforming reactor. The reactor consists of a set of combustion channels and a set of reforming channels in an alternating arrangement. The thermally integrated microchannel reactor is depicted schematically in Figure 1. The straight channels can be configured and manifolded for simultaneous passage of different process reactant streams with flow paths in counter-current, cross-flow, or co-current flow modes [45, 46]. In the present study, the reactor is configured to operate in a co-current flow mode, and each channel contains a layer of catalyst, as depicted schematically in Figure 1. A reactant stream of methanol and air is introduced into the combustion channels and a reactant stream of methanol and steam is introduced into the reforming channels. The flow paths are configured in the reactor to thermally contact exothermic and endothermic reactant streams in adjacent channels.

A high temperature exothermic reaction takes place in the combustion channels and the reforming process reactant stream simultaneously undergoes an endothermic reaction in the reforming channels. No flame combustion is involved in the process. The catalyst layers in each channel are designed in an opposed relationship such that the exothermic heat of reaction taking place within the catalyst layers of the first set of flow channels can be transferred conductively directly through the channel walls to the catalyst layers of the second set of flow channels. The catalytically active surface area or catalyst loading can be balanced between the two sets of channels. In this context, the heat released by the exothermic reaction could be entirely consumed by the endothermic reaction [47, 48], thereby avoiding heat imbalances within the reactor or reducing the likelihood of the formation of hot spots within the catalyst layers, which could sinter or deactivate if exposed to high temperatures.

The temperature of the reactant streams is 373 K at the flow inlets, with a pressure of 2.0 MPa. The equivalence ratio of fuel to air is 0.8 and the steam-to-carbon molar ratio is 1.4. The velocity of the process reactant stream and the combustible reactant stream is 2.0 and 0.6 m/s, respectively, at the flow inlets. The cross-sectional shape of the channels is square, with a side length of 0.7 mm. The channels are 50.0 mm in length. The catalyst layers and the channel walls are 0.1 and 0.7 mm, respectively, in thickness. At room temperature, the thermal conductivity, which indicates the ability to conduct heat, of the channel walls is 200 W/(m·K).

2.2. Mathematical model

The model consists of channel walls with the adjacent combustion and reforming half-channels in a co-current flow configuration. The mathematical model is solved and implemented in ANSYS FLUENT to obtain the problem solution. ANSYS FLUENT permits multi-dimensional modeling of physical and chemical phenomena in the processes, and various modes of heat transfer can be modeled.

The continuity equation is given by

∂( ρ u x ) ∂x + ∂( ρ u y ) ∂y + ∂( ρ u z ) ∂z =0  ，

where x, y, and z are coordinate variables, ρ is the density, and u is the velocity.

The momentum conservation equations can be written as

- ∂p ∂x - ∂ ∂x [ 2 3 μ( ∂ u xx ∂x + ∂ u yx ∂y + ∂ u zx ∂z ) ]+ ∂ ∂x [ μ( ∂ u x ∂x + ∂ u x ∂x ) ]+ ∂ ∂y [ μ( ∂ u x ∂y + ∂ u y ∂x ) ] + ∂ ∂z [ μ( ∂ u x ∂z + ∂ u z ∂x ) ]=0
- ∂p ∂y - ∂ ∂y [ 2 3 μ( ∂ u xy ∂x + ∂ u yy ∂y + ∂ u zy ∂z ) ]+ ∂ ∂x [ μ( ∂ u y ∂x + ∂ u x ∂y ) ]+ ∂ ∂y [ μ( ∂ u y ∂y + ∂ u y ∂y ) ] + ∂ ∂z [ μ( ∂ u y ∂z + ∂ u z ∂y ) ]=0
- ∂p ∂z - ∂ ∂z [ 2 3 μ( ∂ u xz ∂x + ∂ u yz ∂y + ∂ u zz ∂z ) ]+ ∂ ∂x [ μ( ∂ u z ∂x + ∂ u x ∂z ) ]+ ∂ ∂y [ μ( ∂ u z ∂y + ∂ u y ∂z ) ] + ∂ ∂z [ μ( ∂ u z ∂z + ∂ u z ∂z ) ]=0 MathType@MTEF@5@5@+= feaagKart1ev2aaatCvAUfeBSjuyZL2yd9gzLbvyNv2CaerbuLwBLn hiov2DGi1BTfMBaeXatLxBI9gBaerbd9wDYLwzYbItLDharqqtubsr 4rNCHbWexLMBbXgBd9gzLbvyNv2CaeHbl7mZLdGeaGqiVu0Je9sqqr pepC0xbbL8F4rqqrFfpeea0xe9Lq=Jc9vqaqpepm0xbba9pwe9Q8fs 0=yqaqpepae9pg0FirpepeKkFr0xfr=xfr=xb9adbaqaaeGaciGaai aabeqaamaabaabauaakqaabeqaaiaah2cadaWcaaqaaiabgkGi2kaa dchaaeaacqGHciITcaWG6baaaiaah2cadaWcaaqaaiabgkGi2cqaai abgkGi2kaadQhaaaWaamWaaeaadaWcaaqaaiaaikdaaeaacaaIZaaa aiabeY7aTnaabmaabaWaaSaaaeaacqGHciITcaWG1bWaaSbaaSqaai aadIhacaWG6baabeaaaOqaaiabgkGi2kaadIhaaaGaaC4kamaalaaa baGaeyOaIyRaamyDamaaBaaaleaacaWG5bGaamOEaaqabaaakeaacq GHciITcaWG5baaaiaahUcadaWcaaqaaiabgkGi2kaadwhadaWgaaWc baGaamOEaiaadQhaaeqaaaGcbaGaeyOaIyRaamOEaaaaaiaawIcaca GLPaaaaiaawUfacaGLDbaacaWHRaWaaSaaaeaacqGHciITaeaacqGH ciITcaWG4baaamaadmaabaGaeqiVd02aaeWaaeaadaWcaaqaaiabgk Gi2kaadwhadaWgaaWcbaGaamOEaaqabaaakeaacqGHciITcaWG4baa aiaahUcadaWcaaqaaiabgkGi2kaadwhadaWgaaWcbaGaamiEaaqaba aakeaacqGHciITcaWG6baaaaGaayjkaiaawMcaaaGaay5waiaaw2fa aiaahUcadaWcaaqaaiabgkGi2cqaaiabgkGi2kaadMhaaaWaamWaae aacqaH8oqBdaqadaqaamaalaaabaGaeyOaIyRaamyDamaaBaaaleaa caWG6baabeaaaOqaaiabgkGi2kaadMhaaaGaaC4kamaalaaabaGaey OaIyRaamyDamaaBaaaleaacaWG5baabeaaaOqaaiabgkGi2kaadQha aaaacaGLOaGaayzkaaaacaGLBbGaayzxaaaabaGaaC4kamaalaaaba GaeyOaIylabaGaeyOaIyRaamOEaaaadaWadaqaaiabeY7aTnaabmaa baWaaSaaaeaacqGHciITcaWG1bWaaSbaaSqaaiaadQhaaeqaaaGcba GaeyOaIyRaamOEaaaacaWHRaWaaSaaaeaacqGHciITcaWG1bWaaSba aSqaaiaadQhaaeqaaaGcbaGaeyOaIyRaamOEaaaaaiaawIcacaGLPa aaaiaawUfacaGLDbaacaWH9aGaaGimaaaaaa@AB85@

where p is the pressure, and μ is the dynamic viscosity.

The energy conservation equation is given by

∂( ρ u x h ) ∂x + ∂( ρ u y h ) ∂y + ∂( ρ u z h ) ∂z + ∂ ∂x ( ρ ∑ k=1 γ w k h k V k,x - k g ∂T ∂x ) + ∂ ∂y ( ρ ∑ k=1 γ w k h k V k,y - k g ∂T ∂y ) + ∂ ∂z ( ρ ∑ k=1 γ w k h k V k,z - k g ∂T ∂z )=0 MathType@MTEF@5@5@+= feaagKart1ev2aaatCvAUfeBSjuyZL2yd9gzLbvyNv2CaerbuLwBLn hiov2DGi1BTfMBaeXatLxBI9gBaerbd9wDYLwzYbItLDharqqtubsr 4rNCHbWexLMBbXgBd9gzLbvyNv2CaeHbl7mZLdGeaGqiVu0Je9sqqr pepC0xbbL8F4rqqrFfpeea0xe9Lq=Jc9vqaqpepm0xbba9pwe9Q8fs 0=yqaqpepae9pg0FirpepeKkFr0xfr=xfr=xb9adbaqaaeGaciGaai aabeqaamaabaabauaakqaabeqaamaalaaabaGaeyOaIy7aaeWaaeaa cqaHbpGCcaWG1bWaaSbaaSqaaiaadIhaaeqaaOGaamiAaaGaayjkai aawMcaaaqaaiabgkGi2kaadIhaaaGaaC4kamaalaaabaGaeyOaIy7a aeWaaeaacqaHbpGCcaWG1bWaaSbaaSqaaiaadMhaaeqaaOGaamiAaa GaayjkaiaawMcaaaqaaiabgkGi2kaadMhaaaGaaC4kamaalaaabaGa eyOaIy7aaeWaaeaacqaHbpGCcaWG1bWaaSbaaSqaaiaadQhaaeqaaO GaamiAaaGaayjkaiaawMcaaaqaaiabgkGi2kaadQhaaaGaaC4kamaa laaabaGaeyOaIylabaGaeyOaIyRaamiEaaaadaqadaqaaiabeg8aYn aaqahabaGaam4DamaaBaaaleaacaWGRbaabeaakiaadIgadaWgaaWc baGaam4AaaqabaGccaWGwbWaaSbaaSqaaiaadUgacaGGSaGaamiEaa qabaGccaWHTaGaam4AamaaBaaaleaacaWGNbaabeaakmaalaaabaGa eyOaIyRaamivaaqaaiabgkGi2kaadIhaaaaaleaacaWGRbGaaCypai aaigdaaeaacqaHZoWza0GaeyyeIuoaaOGaayjkaiaawMcaaiaahUca daWcaaqaaiabgkGi2cqaaiabgkGi2kaadMhaaaWaaeWaaeaacqaHbp GCdaaeWbqaaiaadEhadaWgaaWcbaGaam4AaaqabaGccaWGObWaaSba aSqaaiaadUgaaeqaaOGaamOvamaaBaaaleaacaWGRbGaaiilaiaadM haaeqaaOGaaCylaiaadUgadaWgaaWcbaGaam4zaaqabaGcdaWcaaqa aiabgkGi2kaadsfaaeaacqGHciITcaWG5baaaaWcbaGaam4Aaiaah2 dacaaIXaaabaGaeq4SdCganiabggHiLdaakiaawIcacaGLPaaaaeaa caWHRaWaaSaaaeaacqGHciITaeaacqGHciITcaWG6baaamaabmaaba GaeqyWdi3aaabCaeaacaWG3bWaaSbaaSqaaiaadUgaaeqaaOGaamiA amaaBaaaleaacaWGRbaabeaakiaadAfadaWgaaWcbaGaam4AaiaacY cacaWG6baabeaakiaah2cacaWGRbWaaSbaaSqaaiaadEgaaeqaaOWa aSaaaeaacqGHciITcaWGubaabaGaeyOaIyRaamOEaaaaaSqaaiaadU gacaWH9aGaaGymaaqaaiabeo7aNbqdcqGHris5aaGccaGLOaGaayzk aaGaaCypaiaaicdaaaaa@B998@

where h is the enthalpy, k is the thermal conductivity, T is the temperature, γ is the total number of gaseous species, w is the mass fraction, and V is the diffusion velocity. The subscripts k and g denote gaseous species k and the gas mixture, respectively.

The species conservation equation can be written as

∂( ρ u x w k ) ∂x  + ∂( ρ u y w k ) ∂y + ∂( ρ u z w k ) ∂z + ∂ ∂x ( ρ w k V k,x ) + ∂ ∂y ( ρ w k V k,y )+ ∂ ∂z ( ρ w k V k,z )- ξ ˙ k W k =0, k=1,…, K g MathType@MTEF@5@5@+= feaagKart1ev2aaatCvAUfeBSjuyZL2yd9gzLbvyNv2CaerbuLwBLn hiov2DGi1BTfMBaeXatLxBI9gBaerbd9wDYLwzYbItLDharqqtubsr 4rNCHbWexLMBbXgBd9gzLbvyNv2CaeHbl7mZLdGeaGqiVu0Je9sqqr pepC0xbbL8F4rqqrFfpeea0xe9Lq=Jc9vqaqpepm0xbba9pwe9Q8fs 0=yqaqpepae9pg0FirpepeKkFr0xfr=xfr=xb9adbaqaaeGaciGaai aabeqaamaabaabauaakqaabeqaamaalaaabaGaeyOaIy7aaeWaaeaa cqaHbpGCcaWG1bWaaSbaaSqaaiaadIhaaeqaaOGaam4DamaaBaaale aacaWGRbaabeaaaOGaayjkaiaawMcaaaqaaiabgkGi2kaadIhaaaGa aGjcVlaahUcadaWcaaqaaiabgkGi2oaabmaabaGaeqyWdiNaamyDam aaBaaaleaacaWG5baabeaakiaadEhadaWgaaWcbaGaam4Aaaqabaaa kiaawIcacaGLPaaaaeaacqGHciITcaWG5baaaiaahUcadaWcaaqaai abgkGi2oaabmaabaGaeqyWdiNaamyDamaaBaaaleaacaWG6baabeaa kiaadEhadaWgaaWcbaGaam4AaaqabaaakiaawIcacaGLPaaaaeaacq GHciITcaWG6baaaiaahUcadaWcaaqaaiabgkGi2cqaaiabgkGi2kaa dIhaaaWaaeWaaeaacqaHbpGCcaWG3bWaaSbaaSqaaiaadUgaaeqaaO GaamOvamaaBaaaleaacaWGRbGaaiilaiaadIhaaeqaaaGccaGLOaGa ayzkaaGaaC4kamaalaaabaGaeyOaIylabaGaeyOaIyRaamyEaaaada qadaqaaiabeg8aYjaadEhadaWgaaWcbaGaam4AaaqabaGccaWGwbWa aSbaaSqaaiaadUgacaGGSaGaamyEaaqabaaakiaawIcacaGLPaaaca WHRaWaaSaaaeaacqGHciITaeaacqGHciITcaWG6baaamaabmaabaGa eqyWdiNaam4DamaaBaaaleaacaWGRbaabeaakiaadAfadaWgaaWcba Gaam4AaiaacYcacaWG6baabeaaaOGaayjkaiaawMcaaiaah2cacuaH +oaEgaGaamaaBaaaleaacaWGRbaabeaakiaadEfadaWgaaWcbaGaam 4AaaqabaGccaWH9aGaaGimaiaacYcaaeaacaWGRbGaaCypaiaaigda caGGSaGaeSOjGSKaaiilaiaadUeadaWgaaWcbaGaam4zaaqabaaaaa a@9C27@

where W is the molecular mass, and ξ ˙ is the rate of production by gas-phase reaction.

The surface species conservation equation is given by

θ m ζ ˙ m Γ -1 =0, ω=γ+1,…,γ+δ  ,
(7)

where θ is the coverage, ω and δ are the total number of chemical species and surface species, respectively, Γ is the active site density, and ζ ˙ is the rate of production by surface reaction. The subscript m denotes surface species m.

The energy conservation equation of the solid phase can be written as

∂ ∂x ( k s ∂T ∂x )+ ∂ ∂y ( k s ∂T ∂y )+ ∂ ∂z ( k s ∂T ∂z )=0  .
(8)

where the subscript s denotes the solid walls.

The surface species conservation equations are given by

ηα W k ( s ˙ k ) ψ + ( ρ w k V k,y ) ψ =0, k=1,…, K g   ,
(9)
ηα W k ( s ˙ k ) ψ + ( ρ w k V k,z ) ψ =0, k=1,…, K g   ,
(10)

in which α is the surface area factor.

The effective diffusivity is defined as

1 D ′ i = 1 ε p τ p ( 1 D i m + 1 D i K )  .
(11)

where εp is the porosity, τp is the tortuosity factor, and Dm and DK are the molecular diffusivity and Knudsen diffusivity, respectively.

The Knudsen diffusivity is defined as

D i K = d 3 ( 8RT ) 1 2 ( π W i ) - 1 2   .
(12)

wherein d is the mean pore diameter.

The effective thermal conductivity k' is defined as

k ′ = ε p k g +( 1- ε p )k  .
(13)

At the solid-gas phase boundaries, the energy conservation equation is given by

k s ( ∂T ∂y ) ψ+ + k s ( ∂T ∂z ) ψ+ + ∑ k=1 K g ( s ˙ k h k W k ) ψ - k g ( ∂T ∂y ) ψ- - k g ( ∂T ∂z ) ψ- =0  .
.(14)
2.3. Chemical kinetic models

The exothermic, catalytic combustion reaction is given by

CH 3 OH + 1 .5O 2  ⇔  2H 2 O +  CO 2  ,   Δ r H m ( 298.15 K )=-726.60 kJ⋅ mol -1   ,
(15)

wherein Δ r H m is the standard molar enthalpy of reaction. Homogeneous combustion is not accounted for, as the desired operating temperatures are low for the reactor.

Methanol can be reformed according to the reactions:

CH 3 OH +  H 2 O ⇔  3H 2  +  CO 2  ,   Δ r H m ( 298.15 K )=49.37 kJ⋅ mol -1   ,
(16)
CH 3 OH ⇔  2H 2  + CO ,  Δ r H m ( 298.15 K )=90.47 kJ⋅ mol -1   .
(17)

The water-gas shift reaction is described by

CO +  H 2 O ⇔  H 2  +  CO 2  ,  Δ r H m ( 298.15 K )=-41.10 kJ⋅ mol -1   .
(18)

The combustion process is modeled by the kinetic model [49], and the reforming process is modeled by the kinetic model [50]. For the reforming reaction, the rate equation can be written as

r decomposition =[ k D K CH 3 O (2) ∗ ( p CH 3 OH p H 2 -0.5 )( 1- k D -1 p H 2 2 p CO p CH 3 OH -1 ) c S 2 T c S 2a T ]       ⋅ [ ( 1+ K CH 3 O (2) ∗ ( p CH 3 OH p H 2 -0.5 )+ K OH (2) ∗ ( p H 2 O p H 2 -0.5 ) )( 1+ K H (2a) 0.5 p H 2 0.5 ) ] -1
(19)

where r is the reaction rate, c S i T is the total surface concentration of site i, K is the equilibrium constant, k is the rate constant, the superscript (i) denotes the species adsorbed on active site i, the superscript * denotes the composite parameter, and the subscripts 1 and 1a denote the species index.

For the water-gas shift reaction, the rate equation can be written as

r water-gas shift =[ k W ∗ K OH (1) ∗ ( p CO p H 2 O p H 2 -0.5 )( 1- k W -1 p H 2 p CO 2 p CO -1 p H 2 O -1 ) c S 1 T 2 ]       ⋅ [ ( 1+ K CH 3 O (1) ∗ ( p CH 3 OH p H 2 -0.5 )+ K HCOO (1) ∗ p CO 2 p H 2 0.5 + K OH (1) ∗ ( p H 2 O p H 2 -0.5 ) ) ] -2 MathType@MTEF@5@5@+= feaagKart1ev2aaatCvAUfeBSjuyZL2yd9gzLbvyNv2CaerbuLwBLn hiov2DGi1BTfMBaeXatLxBI9gBaerbd9wDYLwzYbItLDharqqtubsr 4rNCHbWexLMBbXgBd9gzLbvyNv2CaeHbl7mZLdGeaGqiVu0Je9sqqr pepC0xbbL8F4rqqrFfpeea0xe9Lq=Jc9vqaqpepm0xbba9pwe9Q8fs 0=yqaqpepae9pg0FirpepeKkFr0xfr=xfr=xb9adbaqaaeGaciGaai aabeqaamaabaabauaakqaabaqaaiaadkhadaWgaaWcbaaeaaaaaaaa a8qacaWG3bGaamyyaiaadshacaWGLbGaamOCaiaah2cacaWGNbGaam yyaiaadohacaqGGaGaam4CaiaadIgacaWGPbGaamOzaiaadshaa8aa beaakiaah2dadaWadaqaaiaadUgadaqhaaWcbaGaam4vaaqaaiabgE HiQaaakiaadUeadaqhaaWcbaGaae4taiaabIeadaahaaadbeqaaiaa bIcacaqGXaGaaeykaaaaaSqaaiabgEHiQaaakmaabmaabaGaamiCam aaBaaaleaacaqGdbGaae4taaqabaGccaWGWbWaaSbaaSqaaiaabIea daWgaaadbaGaaeOmaaqabaWccaqGpbaabeaakiaadchadaqhaaWcba GaaeisamaaBaaameaacaqGYaaabeaaaSqaaiaah2cacaaIWaGaaiOl aiaaiwdaaaaakiaawIcacaGLPaaadaqadaqaaiaabgdacaWHTaGaam 4AamaaDaaaleaacaWGxbaabaGaaCylaiaaigdaaaGccaWGWbWaaSba aSqaaiaabIeadaWgaaadbaGaaeOmaaqabaaaleqaaOGaamiCamaaBa aaleaacaqGdbGaae4tamaaBaaameaacaqGYaaabeaaaSqabaGccaWG WbWaa0baaSqaaiaaboeacaqGpbaabaGaaCylaiaaigdaaaGccaWGWb Waa0baaSqaaiaabIeadaWgaaadbaGaaeOmaaqabaWccaqGpbaabaGa aCylaiaaigdaaaaakiaawIcacaGLPaaacaWGJbWaa0baaSqaaiaado fadaWgaaadbaGaaGymaaqabaaaleaacaWGubWaaWbaaWqabeaacaaI YaaaaaaaaOGaay5waiaaw2faaaqaaiaabccacaqGGaGaaeiiaiaabc cacaqGGaGaaeiiaiabgwSixpaadmaabaWaaeWaaeaacaqGXaGaaC4k aiaadUeadaqhaaWcbaGaae4qaiaabIeadaWgaaadbaGaae4maaqaba WccaqGpbWaaWbaaWqabeaacaqGOaGaaeymaiaabMcaaaaaleaacqGH xiIkaaGcdaqadaqaaiaadchadaWgaaWcbaGaae4qaiaabIeadaWgaa adbaGaae4maaqabaWccaqGpbGaaeisaaqabaGccaWGWbWaa0baaSqa aiaabIeadaWgaaadbaGaaeOmaaqabaaaleaacaWHTaGaaGimaiaac6 cacaaI1aaaaaGccaGLOaGaayzkaaGaaC4kaiaadUeadaqhaaWcbaGa aeisaiaaboeacaqGpbGaae4tamaaCaaameqabaGaaeikaiaabgdaca qGPaaaaaWcbaGaey4fIOcaaOGaamiCamaaBaaaleaacaqGdbGaae4t amaaBaaameaacaqGYaaabeaaaSqabaGccaWGWbWaa0baaSqaaiaabI eadaWgaaadbaGaaeOmaaqabaaaleaacaaIWaGaaiOlaiaaiwdaaaGc caWHRaGaam4samaaDaaaleaacaqGpbGaaeisamaaCaaameqabaGaae ikaiaabgdacaqGPaaaaaWcbaGaey4fIOcaaOWaaeWaaeaacaWGWbWa aSbaaSqaaiaabIeadaWgaaadbaGaaeOmaaqabaWccaqGpbaabeaaki aadchadaqhaaWcbaGaaeisamaaBaaameaacaqGYaaabeaaaSqaaiaa h2cacaaIWaGaaiOlaiaaiwdaaaaakiaawIcacaGLPaaaaiaawIcaca GLPaaaaiaawUfacaGLDbaadaahaaWcbeqaaiaah2cacaaIYaaaaaaa aa@C591@
(20)

For the decomposition reaction, the rate equation can be written as

r decomposition =[ k D K CH 3 O (2) ∗ ( p CH 3 OH p H 2 -0.5 )( 1- k D -1 p H 2 2 p CO p CH 3 OH -1 ) c S 2 T c S 2a T ]       ⋅ [ ( 1+ K CH 3 O (2) ∗ ( p CH 3 OH p H 2 -0.5 )+ K OH (2) ∗ ( p H 2 O p H 2 -0.5 ) )( 1+ K H (2a) 0.5 p H 2 0.5 ) ] -1 MathType@MTEF@5@5@+= feaagKart1ev2aaatCvAUfeBSjuyZL2yd9gzLbvyNv2CaerbuLwBLn hiov2DGi1BTfMBaeXatLxBI9gBaerbd9wDYLwzYbItLDharqqtubsr 4rNCHbWexLMBbXgBd9gzLbvyNv2CaeHbl7mZLdGeaGqiVu0Je9sqqr pepC0xbbL8F4rqqrFfpeea0xe9Lq=Jc9vqaqpepm0xbba9pwe9Q8fs 0=yqaqpepae9pg0FirpepeKkFr0xfr=xfr=xb9adbaqaaeGaciGaai aabeqaamaabaabauaakqaabaqaaiaadkhadaWgaaWcbaaeaaaaaaaa a8qacaWGKbGaamyzaiaadogacaWGVbGaamyBaiaadchacaWGVbGaam 4CaiaadMgacaWG0bGaamyAaiaad+gacaWGUbaapaqabaGccaWH9aWa amWaaeaacaWGRbWaaSbaaSqaaiaadseaaeqaaOGaam4samaaDaaale aacaqGdbGaaeisamaaBaaameaacaqGZaaabeaaliaab+eadaahaaad beqaaiaabIcacaqGYaGaaeykaaaaaSqaaiabgEHiQaaakmaabmaaba GaamiCamaaBaaaleaacaqGdbGaaeisamaaBaaameaacaqGZaaabeaa liaab+eacaqGibaabeaakiaadchadaqhaaWcbaGaaeisamaaBaaame aacaqGYaaabeaaaSqaaiaah2cacaaIWaGaaiOlaiaaiwdaaaaakiaa wIcacaGLPaaadaqadaqaaiaabgdacaWHTaGaam4AamaaDaaaleaaca WGebaabaGaaCylaiaaigdaaaGccaWGWbWaa0baaSqaaiaabIeadaWg aaadbaGaaeOmaaqabaaaleaacaaIYaaaaOGaamiCamaaBaaaleaaca qGdbGaae4taaqabaGccaWGWbWaa0baaSqaaiaaboeacaqGibWaaSba aWqaaiaabodaaeqaaSGaae4taiaabIeaaeaacaWHTaGaaGymaaaaaO GaayjkaiaawMcaaiaadogadaqhaaWcbaGaam4uamaaBaaameaacaaI YaaabeaaaSqaaiaadsfaaaGccaWGJbWaa0baaSqaaiaadofadaWgaa adbaGaaGOmaiaadggaaeqaaaWcbaGaamivaaaaaOGaay5waiaaw2fa aaqaaiaabccacaqGGaGaaeiiaiaabccacaqGGaGaaeiiaiabgwSixp aadmaabaWaaeWaaeaacaqGXaGaaC4kaiaadUeadaqhaaWcbaGaae4q aiaabIeadaWgaaadbaGaae4maaqabaWccaqGpbWaaWbaaWqabeaaca qGOaGaaeOmaiaabMcaaaaaleaacqGHxiIkaaGcdaqadaqaaiaadcha daWgaaWcbaGaae4qaiaabIeadaWgaaadbaGaae4maaqabaWccaqGpb GaaeisaaqabaGccaWGWbWaa0baaSqaaiaabIeadaWgaaadbaGaaeOm aaqabaaaleaacaWHTaGaaGimaiaac6cacaaI1aaaaaGccaGLOaGaay zkaaGaaC4kaiaadUeadaqhaaWcbaGaae4taiaabIeadaahaaadbeqa aiaabIcacaqGYaGaaeykaaaaaSqaaiabgEHiQaaakmaabmaabaGaam iCamaaBaaaleaacaqGibWaaSbaaWqaaiaabkdaaeqaaSGaae4taaqa baGccaWGWbWaa0baaSqaaiaabIeadaWgaaadbaGaaeOmaaqabaaale aacaWHTaGaaGimaiaac6cacaaI1aaaaaGccaGLOaGaayzkaaaacaGL OaGaayzkaaWaaeWaaeaacaqGXaGaaC4kaiaadUeadaqhaaWcbaGaae isamaaCaaameqabaGaaiikaiaaikdacaWGHbGaaiykaaaaaSqaaiaa icdacaGGUaGaaGynaaaakiaadchadaqhaaWcbaGaaeisamaaBaaame aacaqGYaaabeaaaSqaaiaaicdacaGGUaGaaGynaaaaaOGaayjkaiaa wMcaaaGaay5waiaaw2faamaaCaaaleqabaGaaCylaiaaigdaaaaaaa a@C2E5@
(21)

where the subscripts 2 and 2a denote the species index.

2.4. Numerical methods

The computational domain is divided into discrete control volumes using a computational grid. The typical mesh consists of about 600,000 nodes in total. The governing equations are integrated on the individual control volumes to construct algebraic equations for the discrete dependent variables such as temperature, pressure, velocities, and conserved scalars. The discretized equations are linearized and the resultant linear equation system is solved to yield updated values of the dependent variables. The constraint of mass conservation of the velocity field is achieved by solving a pressure equation. The pressure equation is derived from the mass and momentum conservation equations in such a way that the velocity field, corrected by the pressure, satisfies the continuity. The second-order upwind spatial discretization scheme is used for the convection terms of each governing equation. Pressure-velocity coupling is achieved by using the standard SIMPLE algorithm. The under-relaxation parameters are reduced for all variables. Convergence is judged by examining residual levels.

2.5. Validation of the model

To verify the accuracy of the model, the predictions are compared with the data obtained from experimental measurements [51, 52]. The cross-sectional shape of the channels is rectangular. The channels have a height of 0.6 mm, a width of 0.5 mm, and a length of 33.0 mm. The reaction temperature varies from 473 to 533 K. The steam-to-carbon molar ratio is 1.1 for the reforming process. The methanol conversion and hydrogen production rate are plotted in Figure 3 against temperature. The predictions are in satisfactory agreement with the data obtained from experimental measurements.

Figure 2
(a) Methanol conversion and (b) hydrogen production rate at different reaction temperatures. The experimental data [51, 52] are included for comparison.

4. Results and discussion

4.1. Overall heat transfer characteristics

The contour plots of temperature, enthalpy, and sensible enthalpy are illustrated in Figure 3 for the reactor. The thermal energy released from the combustion channels is conducted through the channel walls to reforming channels, thereby supporting the endothermic conversion reaction. The thermal conductivity of the channel walls is high so as to facilitate the efficient transfer of thermal energy from the combustion channels to the reforming channels, as illustrated in Figure 3. To enhance heat transfer within the reactor by dramatically increasing heat transfer area, the flow channels could contain internal, function fins [53], for example, castellated walls, saw tooth walls, or any other type of walls [54], such as grooved, serpentine or any other design. The geometry and dimensions of the flow channels may vary depending upon the design parameters of the reaction system [55, 56].

Figure 3
Contour plots of temperature, specific enthalpy, and specific sensible enthalpy for the reactor. The channels are square in cross section. At room temperature, the thermal conductivity of the channel walls is 200 W/(m·K).

The temperature rises very quickly in the reactor, as illustrated in Figure 3, reaching about 560 K at which the structural integrity of the reactor might be compromised. High temperatures would potentially destroy or deactivate the catalyst layers of the reactor and may pose a risk to the structural integrity of the reactor. Within the channel walls, a substantially uniform temperature profile is achieved, as illustrated in Figure 3, because of the excellent heat conduction properties of the channel walls, which can improve the performance of the reaction system with increased conversion due to their high thermal conductivity. The contour plots of species mole fractions are illustrated in Figure 4 for the reactor. Nearly complete conversion to hydrogen is achieved and the rate of conversion is high due to the excellent heat conduction properties of the channel walls.

Figure 4
Contour plots of species mole fractions for the reactor. At room temperature, the thermal conductivity of the channel walls is 200 W/(m·K).

Instead of temperature, a change in enthalpy or sensible enthalpy can be used as the state variable to account for simplifying the description of heat transfer. For the mixtures, the enthalpy correlates to their thermal energy. The change in enthalpy for the reforming process is the heat absorbed by the endothermic reactant stream. The change in enthalpy for the combustion process is the heat released by the exothermic reactant stream. There is a significant change in specific enthalpy or specific sensible enthalpy along the streamwise direction, as illustrated in Figure 3, especially near the channel inlets. Accordingly, the conversion occurs very rapidly near the channel inlets and almost complete conversion is achieved, as illustrated in Figure 4. This is because excellent wall heat conduction properties tend to facilitate the conversion.

For the exothermic catalytic combustion reaction, the change in total enthalpy is negative, since the total enthalpy of combustion products is smaller than that of the reactants of the reaction. The change in total enthalpy is equal to the heat released by the exothermic reaction. For the endothermic steam reforming reaction, the change in total enthalpy is positive, since the total enthalpy of reforming products is larger than that of the reactants of the reaction. The change in total enthalpy is equal to the heat absorbed by the endothermic reaction. However, these results can be applied only to total enthalpy. When applied to specific enthalpy, the change in specific enthalpy is positive for the exothermic catalytic combustion reaction and the change in specific enthalpy is negative for the endothermic steam reforming reaction, as illustrated in Figure 3. However, the change in specific sensible enthalpy is always positive, especially for the exothermic process. This is because the temperature of the streams will continue to rise along the streamwise direction due to the heat released by the combustion reaction. On the other hand, the concentration of species has a steep gradient in the flow channels, as illustrated in Figure 4, especially near the channel inlets. This is caused by the small dimensions of the parallel channels and the high rates of the reactions. From an economic standpoint, it is desirable to minimize capital cost while preserving conversion yields through process intensification.

4.2. Effect of wall heat conduction properties

The effect of wall heat conduction properties on the temperature field within the reactor is investigated. The results are presented in Figure 5, in which the two-dimensional contour plots of temperature are illustrated for the reactor. The thermal conductivity of the channel walls varies from 0.2 to 200 W/(m·K). The temperature increases with decreasing the wall thermal conductivity. For the reactor, the desired reaction temperatures can influence the choice of channel wall material. For example, when chosen for the channel walls, the material should not impede on the transport of thermal energy between the endothermic and exothermic streams within the reactor, in addition to a suitable melting point. Within the channel walls, a substantially uniform temperature profile is achieved in the case of a high thermal conductivity of 200 W/(m·K). For example, the excellent heat conduction properties enable a more uniform distribution of temperature along the streamwise direction. This causes a reduction of peak temperature within the reactor, thereby ensuring the structural integrity of the reaction system and prolonging the life of the catalytically active materials. Therefore, the channel walls of the reactor must be formed using materials with excellent heat conduction properties. In this context, thermally conductive ceramics and metals are well-suited, since materials with high thermal conductivity are preferred for the channel walls.

Figure 5
Two-dimensional contour plots of temperature for the reactor. The thermal conductivity of the channel walls varies from 0.2 to 200 W/(m·K).

The effect of wall heat conduction properties on methanol conversion is investigated. The results are presented in Figure 6, in which methanol conversion is plotted against the thermal conductivity of the channel walls. The wall thermal conductivity varies from 0.2 to 200 W/(m·K). As the wall thermal conductivity increases, methanol conversion increases. Wall materials with poor heat conduction properties degrade the reactor performance. Therefore, materials with excellent heat conduction properties are preferred for the reaction system, as discussed above. The channel wall material should be selected with a thermal conductivity at least higher than 20 W/(m·K). For example, copper can be employed as the channel wall material because of it very high thermal conductivity. Even at room temperature, the thermal conductivity of copper can be as high as about 400 W/(m·K), thereby preventing the formation of hot spots. Additionally, this metal material is cost effective.

Figure 6
Two-dimensional contour plots of temperature for the reactor. The thermal conductivity of the channel walls varies from 0.2 to 200 W/(m·K).
4.3. Reaction heat fluxes

The reaction heat fluxes are investigated to better understand the thermal coupling between the endothermic and exothermic streams. The results are presented in Figure 7, in which the endothermic and exothermic reaction heat fluxes are plotted against the streamwise distance. The channels are 0.7 mm in width. The exothermic catalytic combustion reaction provides the necessary heat flux to increase the temperature of the reactants in both channels such that the endothermic reaction will occur. Heat flux is a vector quantity, and therefore the heat flux is negative for the endothermic steam reforming reaction. The exothermic heat flux is greater than the absolute value of the endothermic heat flux. The peak exothermic heat flux is located upstream of the peak endothermic heat flux. An un-uniform catalyst distribution could be employed for the rector so as to provide optimum synchronization of the reaction fluxes of heat consumption and generation in the endothermic reforming and exothermic combustion channels, respectively.

Figure 7
Endothermic and exothermic reaction heat fluxes as a function of the streamwise distance. The channels are 0.7 mm in width.

The effect of channel dimensions on endothermic and exothermic reaction heat fluxes is illustrated in Figure 8. Modifications and variations are made by increasing the dimensions of the channels. The channel dimensions are important factors in practical applications [57, 58]. The channels are 0.7 and 2.0 mm, respectively, in width, but the flow rate remains constant for each process. The evolution of the reaction heat fluxes is illustrated for the two cases. The location of the reaction heat flux peak shifts in channel dimensions. More specifically, as the channel dimensions increase while maintaining the flow rates, the peak of the reaction heat fluxes shifts upstream, causing an increase in the peak reaction heat flux. Intuitively, as the channel dimensions decrease while maintaining the flow rates, the peak of the reaction heat fluxes will shift downstream.

Figure 8
Effect of channel dimensions on endothermic and exothermic reaction heat fluxes. The channels are 0.7 and 2.0 mm, respectively, in width.

6. Conclusions

Computational fluid dynamics simulations are conducted to better understand the consumption, generation, and exchange of thermal energy between endothermic and exothermic processes in a thermally integrated microchannel reforming reactor. The effects of wall heat conduction properties and channel dimensions on heat transfer characteristics and reactor performance are investigated. The major conclusions are summarized as follows:

  • The change in specific enthalpy is positive for the exothermic reaction and negative for the endothermic reaction.
  • The change in specific sensible enthalpy is always positive, especially for the exothermic process.
  • The thermal conductivity of the channel walls is fundamentally important.
  • Materials with high thermal conductivity are preferred for the channel walls. Thermally conductive ceramics and metals are well-suited.
  • Wall materials with poor heat conduction properties degrade the reactor performance. Materials with low thermal conductivity pose a risk to the structural integrity of the reactor and reduce the life of the catalysts.
  • Reaction heat flux profiles are considerably affected by channel dimensions. The peak reaction heat flux increases with the channel dimensions while maintaining the flow rates.

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  38. A. Gavriilidis, P. Angeli, E. Cao, K.K. Yeong, and Y.S.S. Wan. Technology and applications of microengineered reactors. Chemical Engineering Research and Design, Volume 80, Issue 1, 2002, Pages 3-30.[CrossRef]
  39. M.S. Mettler, G.D. Stefanidis, and D.G. Vlachos. Enhancing stability in parallel plate microreactor stacks for syngas production. Chemical Engineering Science, Volume 66, Issue 6, 2011, Pages 1051-1059.[CrossRef]
  40. C. Cao, N. Zhang, D. Dang, and Y. Cheng. Numerical evaluation of a microchannel methane reformer used for miniaturized GTL: Operating characteristics and greenhouse gases emission. Fuel Processing Technology, Volume 167, 2017, Pages 78-91.[CrossRef]
  41. J.J. Lerou, A.L. Tonkovich, L. Silva, S. Perry, and J. McDaniel. Microchannel reactor architecture enables greener processes. Chemical Engineering Science, Volume 65, Issue 1, 2010, Pages 380-385.[CrossRef]
  42. D.M. Murphy, A. Manerbino, M. Parker, J. Blasi, R.J. Kee, and N.P. Sullivan. Methane steam reforming in a novel ceramic microchannel reactor. International Journal of Hydrogen Energy, Volume 38, Issue 21, 2013, Pages 8741-8750.[CrossRef]
  43. M. Baldea and P. Daoutidis. Dynamics and control of autothermal reactors for the production of hydrogen. Chemical Engineering Science, Volume 62, Issue 12, 2007, Pages 3218-3230.[CrossRef]
  44. M. Zanfir and A. Gavriilidis. Influence of flow arrangement in catalytic plate reactors for methane steam reforming. Chemical Engineering Research and Design, Volume 82, Issue 2, 2004, Pages 252-258.[CrossRef]
  45. G. Kolios, J. Frauhammer, and G. Eigenberger. Autothermal fixed-bed reactor concepts. Chemical Engineering Science, Volume 55, Issue 24, 2000, Pages 5945-5967.[CrossRef]
  46. T.P. Tiemersma, T. Kolkman, J.A.M. Kuipers, and M.V.S. Annaland. A novel autothermal reactor concept for thermal coupling of the exothermic oxidative coupling and endothermic steam reforming of methane. Chemical Engineering Journal, Volume 203, 2012, Pages 223-230.[CrossRef]
  47. M.S. Herdem, M. Mundhwa, S. Farhad, and F. Hamdullahpur. Catalyst layer design and arrangement to improve the performance of a microchannel methanol steam reformer. Energy Conversion and Management, Volume 180, 2019, Pages 149-161.[CrossRef]
  48. N. Engelbrecht, R.C. Everson, D. Bessarabov, and G. Kolb. Microchannel reactor heat-exchangers: A review of design strategies for the effective thermal coupling of gas phase reactions. Chemical Engineering and Processing - Process Intensification, Volume 157, 2020, Article Number: 108164.[CrossRef]
  49. T.L. Reitz, S. Ahmed, M. Krumpelt, R. Kumar, and H.H. Kung. Characterization of CuO/ZnO under oxidizing conditions for the oxidative methanol reforming reaction. Journal of Molecular Catalysis A: Chemical, Volume 162, Issues 1-2, 2000, Pages 275-285.[CrossRef]
  50. B.A. Peppley, J.C. Amphlett, L.M. Kearns, and R.F. Mann. Methanol-steam reforming on Cu/ZnO/Al2O3 catalysts. Part 2. A comprehensive kinetic model. Applied Catalysis A: General, Volume 179, Issues 1-2, 1999, Pages 31-49.[CrossRef]
  51. G.-G. Park, D.J. Seo, S.-H. Park, Y.-G. Yoon, C.-S. Kim, and W.-L. Yoon. Development of microchannel methanol steam reformer. Chemical Engineering Journal, Volume 101, Issues 1-3, 2004, Pages 87-92.[CrossRef]
  52. G.-G. Park, S.-D. Yim, Y.-G. Yoon, C.-S. Kim, D.-J. Seo, and K. Eguchi. Hydrogen production with integrated microchannel fuel processor using methanol for portable fuel cell systems. Catalysis Today, Volume 110, Issues 1-2, 2005, Pages 108-113.[CrossRef]
  53. X. Chu, X. Zeng, T. Zheng, W. Zhuang, Y. Yang, W. Zhou, and Y. Hong. Structural design and performance research of methanol steam reforming microchannel for hydrogen production based on mixing effect. International Journal of Hydrogen Energy, Volume 45, Issue 41, 2020, Pages 20859-20874.[CrossRef]
  54. W. Lu, R. Zhang, S. Toan, R. Xu, F. Zhou, Z. Sun, and Z. Sun. Microchannel structure design for hydrogen supply from methanol steam reforming. Chemical Engineering Journal, Volume 429, 2022, Article Number: 132286.[CrossRef]
  55. G.D. Stefanidis, D.G. Vlachos, N.S. Kaisare, and M. Maestri. Methane steam reforming at microscales: Operation strategies for variable power output at millisecond contact times. AIChE Journal, Volume 55, Issue 1, 2009, Pages 180-191.[CrossRef]
  56. G.D. Stefanidis and D.G. Vlachos. Millisecond methane steam reforming via process and catalyst intensification. Chemical Engineering & Technology, Volume 31, Issue 8, 2008, Pages 1201-1209.[CrossRef]
  57. M. Zanfir and A. Gavriilidis. Catalytic combustion assisted methane steam reforming in a catalytic plate reactor. Chemical Engineering Science, Volume 58, Issue 17, 2003, Pages 3947-3960.[CrossRef]
  58. C. Cao, D. Dang, Y. Li, J. Xu, and Y. Cheng. Managing temperature uniformity of thermally integrated micro reformers with different axial dimensions: A detailed numerical study. Chemical Engineering and Processing - Process Intensification, Volume 132, 2018, Pages 218-228.[CrossRef]
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APA Style
Chen, J. (2022). Computational Fluid Dynamics Modeling of Thermally Integrated Microchannel Reforming Reactors for Hydrogen Production. Online Journal of Engineering Sciences, 1(1), 29-44. https://doi.org/10.31586/ojes.2022.228
ACS Style
Chen, J. Computational Fluid Dynamics Modeling of Thermally Integrated Microchannel Reforming Reactors for Hydrogen Production. Online Journal of Engineering Sciences 2022 1(1), 29-44. https://doi.org/10.31586/ojes.2022.228
Chicago/Turabian Style
Chen, Junjie. 2022. "Computational Fluid Dynamics Modeling of Thermally Integrated Microchannel Reforming Reactors for Hydrogen Production". Online Journal of Engineering Sciences 1, no. 1: 29-44. https://doi.org/10.31586/ojes.2022.228
AMA Style
Chen J. Computational Fluid Dynamics Modeling of Thermally Integrated Microchannel Reforming Reactors for Hydrogen Production. Online Journal of Engineering Sciences. 2022; 1(1):29-44. https://doi.org/10.31586/ojes.2022.228 
@Article{ojes228,
AUTHOR = {Chen, Junjie},
TITLE = {Computational Fluid Dynamics Modeling of Thermally Integrated Microchannel Reforming Reactors for Hydrogen Production},
JOURNAL = {Online Journal of Engineering Sciences},
VOLUME = {1},
YEAR = {2022},
NUMBER = {1},
PAGES = {29-44},
URL = {/10.31586/ojes-1-1-310.31586/ojes/1/1/3},
ISSN = {2833-0145},
DOI = {10.31586/ojes.2022.228},
ABSTRACT = {Many attempts have been made to improve heat transfer for thermally integrated microchannel reforming reactors. However, the mechanisms for the effects of design factors on heat transfer characteristics are still not fully understood. This study relates to a thermochemical process for producing hydrogen by the catalytic endothermic reaction of methanol with steam in a thermally integrated microchannel reforming reactor. Computational fluid dynamics simulations are conducted to better understand the consumption, generation, and exchange of thermal energy between endothermic and exothermic processes in the reactor. The effects of wall heat conduction properties and channel dimensions on heat transfer characteristics and reactor performance are investigated. Thermodynamic analysis is performed based on specific enthalpy to better understand the evolution of thermal energy in the reactor. The results indicate that the thermal conductivity of the channel walls is fundamentally important. Materials with high thermal conductivity are preferred for the channel walls. Thermally conductive ceramics and metals are well-suited. Wall materials with poor heat conduction properties degrade the reactor performance. Reaction heat flux profiles are considerably affected by channel dimensions. The peak reaction heat flux increases with the channel dimensions while maintaining the flow rates. The change in specific enthalpy is positive for the exothermic reaction and negative for the endothermic reaction. The change in specific sensible enthalpy is always positive. Design recommendations are made to improve thermal performance for the reactor.},
}
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%J Online Journal of Engineering Sciences

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%N 1
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%M doi:10.31586/ojes.2022.228
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TY  - JOUR
AU  - Chen, Junjie
TI  - Computational Fluid Dynamics Modeling of Thermally Integrated Microchannel Reforming Reactors for Hydrogen Production
T2  - Online Journal of Engineering Sciences
PY  - 2022
VL  - 1
IS  - 1
SN  - 2833-0145
SP  - 29
EP  - 44
UR  - /10.31586/ojes-1-1-310.31586/ojes/1/1/3
AB  - Many attempts have been made to improve heat transfer for thermally integrated microchannel reforming reactors. However, the mechanisms for the effects of design factors on heat transfer characteristics are still not fully understood. This study relates to a thermochemical process for producing hydrogen by the catalytic endothermic reaction of methanol with steam in a thermally integrated microchannel reforming reactor. Computational fluid dynamics simulations are conducted to better understand the consumption, generation, and exchange of thermal energy between endothermic and exothermic processes in the reactor. The effects of wall heat conduction properties and channel dimensions on heat transfer characteristics and reactor performance are investigated. Thermodynamic analysis is performed based on specific enthalpy to better understand the evolution of thermal energy in the reactor. The results indicate that the thermal conductivity of the channel walls is fundamentally important. Materials with high thermal conductivity are preferred for the channel walls. Thermally conductive ceramics and metals are well-suited. Wall materials with poor heat conduction properties degrade the reactor performance. Reaction heat flux profiles are considerably affected by channel dimensions. The peak reaction heat flux increases with the channel dimensions while maintaining the flow rates. The change in specific enthalpy is positive for the exothermic reaction and negative for the endothermic reaction. The change in specific sensible enthalpy is always positive. Design recommendations are made to improve thermal performance for the reactor.
DO  - Computational Fluid Dynamics Modeling of Thermally Integrated Microchannel Reforming Reactors for Hydrogen Production
TI  - 10.31586/ojes.2022.228
ER  -
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  37. A. Tonkovich, D. Kuhlmann, A. Rogers, J. McDaniel, S. Fitzgerald, R. Arora, and T. Yuschak. Microchannel technology scale-up to commercial capacity. Chemical Engineering Research and Design, Volume 83, Issue 6, 2005, Pages 634-639.[CrossRef]
  38. A. Gavriilidis, P. Angeli, E. Cao, K.K. Yeong, and Y.S.S. Wan. Technology and applications of microengineered reactors. Chemical Engineering Research and Design, Volume 80, Issue 1, 2002, Pages 3-30.[CrossRef]
  39. M.S. Mettler, G.D. Stefanidis, and D.G. Vlachos. Enhancing stability in parallel plate microreactor stacks for syngas production. Chemical Engineering Science, Volume 66, Issue 6, 2011, Pages 1051-1059.[CrossRef]
  40. C. Cao, N. Zhang, D. Dang, and Y. Cheng. Numerical evaluation of a microchannel methane reformer used for miniaturized GTL: Operating characteristics and greenhouse gases emission. Fuel Processing Technology, Volume 167, 2017, Pages 78-91.[CrossRef]
  41. J.J. Lerou, A.L. Tonkovich, L. Silva, S. Perry, and J. McDaniel. Microchannel reactor architecture enables greener processes. Chemical Engineering Science, Volume 65, Issue 1, 2010, Pages 380-385.[CrossRef]
  42. D.M. Murphy, A. Manerbino, M. Parker, J. Blasi, R.J. Kee, and N.P. Sullivan. Methane steam reforming in a novel ceramic microchannel reactor. International Journal of Hydrogen Energy, Volume 38, Issue 21, 2013, Pages 8741-8750.[CrossRef]
  43. M. Baldea and P. Daoutidis. Dynamics and control of autothermal reactors for the production of hydrogen. Chemical Engineering Science, Volume 62, Issue 12, 2007, Pages 3218-3230.[CrossRef]
  44. M. Zanfir and A. Gavriilidis. Influence of flow arrangement in catalytic plate reactors for methane steam reforming. Chemical Engineering Research and Design, Volume 82, Issue 2, 2004, Pages 252-258.[CrossRef]
  45. G. Kolios, J. Frauhammer, and G. Eigenberger. Autothermal fixed-bed reactor concepts. Chemical Engineering Science, Volume 55, Issue 24, 2000, Pages 5945-5967.[CrossRef]
  46. T.P. Tiemersma, T. Kolkman, J.A.M. Kuipers, and M.V.S. Annaland. A novel autothermal reactor concept for thermal coupling of the exothermic oxidative coupling and endothermic steam reforming of methane. Chemical Engineering Journal, Volume 203, 2012, Pages 223-230.[CrossRef]
  47. M.S. Herdem, M. Mundhwa, S. Farhad, and F. Hamdullahpur. Catalyst layer design and arrangement to improve the performance of a microchannel methanol steam reformer. Energy Conversion and Management, Volume 180, 2019, Pages 149-161.[CrossRef]
  48. N. Engelbrecht, R.C. Everson, D. Bessarabov, and G. Kolb. Microchannel reactor heat-exchangers: A review of design strategies for the effective thermal coupling of gas phase reactions. Chemical Engineering and Processing - Process Intensification, Volume 157, 2020, Article Number: 108164.[CrossRef]
  49. T.L. Reitz, S. Ahmed, M. Krumpelt, R. Kumar, and H.H. Kung. Characterization of CuO/ZnO under oxidizing conditions for the oxidative methanol reforming reaction. Journal of Molecular Catalysis A: Chemical, Volume 162, Issues 1-2, 2000, Pages 275-285.[CrossRef]
  50. B.A. Peppley, J.C. Amphlett, L.M. Kearns, and R.F. Mann. Methanol-steam reforming on Cu/ZnO/Al2O3 catalysts. Part 2. A comprehensive kinetic model. Applied Catalysis A: General, Volume 179, Issues 1-2, 1999, Pages 31-49.[CrossRef]
  51. G.-G. Park, D.J. Seo, S.-H. Park, Y.-G. Yoon, C.-S. Kim, and W.-L. Yoon. Development of microchannel methanol steam reformer. Chemical Engineering Journal, Volume 101, Issues 1-3, 2004, Pages 87-92.[CrossRef]
  52. G.-G. Park, S.-D. Yim, Y.-G. Yoon, C.-S. Kim, D.-J. Seo, and K. Eguchi. Hydrogen production with integrated microchannel fuel processor using methanol for portable fuel cell systems. Catalysis Today, Volume 110, Issues 1-2, 2005, Pages 108-113.[CrossRef]
  53. X. Chu, X. Zeng, T. Zheng, W. Zhuang, Y. Yang, W. Zhou, and Y. Hong. Structural design and performance research of methanol steam reforming microchannel for hydrogen production based on mixing effect. International Journal of Hydrogen Energy, Volume 45, Issue 41, 2020, Pages 20859-20874.[CrossRef]
  54. W. Lu, R. Zhang, S. Toan, R. Xu, F. Zhou, Z. Sun, and Z. Sun. Microchannel structure design for hydrogen supply from methanol steam reforming. Chemical Engineering Journal, Volume 429, 2022, Article Number: 132286.[CrossRef]
  55. G.D. Stefanidis, D.G. Vlachos, N.S. Kaisare, and M. Maestri. Methane steam reforming at microscales: Operation strategies for variable power output at millisecond contact times. AIChE Journal, Volume 55, Issue 1, 2009, Pages 180-191.[CrossRef]
  56. G.D. Stefanidis and D.G. Vlachos. Millisecond methane steam reforming via process and catalyst intensification. Chemical Engineering & Technology, Volume 31, Issue 8, 2008, Pages 1201-1209.[CrossRef]
  57. M. Zanfir and A. Gavriilidis. Catalytic combustion assisted methane steam reforming in a catalytic plate reactor. Chemical Engineering Science, Volume 58, Issue 17, 2003, Pages 3947-3960.[CrossRef]
  58. C. Cao, D. Dang, Y. Li, J. Xu, and Y. Cheng. Managing temperature uniformity of thermally integrated micro reformers with different axial dimensions: A detailed numerical study. Chemical Engineering and Processing - Process Intensification, Volume 132, 2018, Pages 218-228.[CrossRef]