Skip to main content

Hydrodeoxygenation of cracked vegetable oil using CoMo/Al2O3 and Pt/C catalysts

Abstract

During the continuous catalytic hydrodeoxygenation (HDO) of cracked vegetable oil (CVO), CO2 and CO occur as the main reaction gases, in addition to hydrocarbon gases such as CH4 and C2H6. The catalysts used were cobalt-molybdenum (CoMo) on an Al2O3 support and platinum (Pt) on an active carbon. All named gas components can result directly from the decomposition of CVO. The results of batch experiments for gas phase reactions (GPRs) under the same 50 bar H2 atmosphere using the same catalysts (CoMo, Pt) indicate that CO and CH4 can also be formed by GPRs. CO can result from the reverse water–gas shift reaction (RWGS), and CH4 from CO- or CO2-methanation. The found CO-yields from GPRs are within the theoretical thermodynamic limits based on equilibrium. An unexpected inhomogeneity of the gas component concentrations in the reactor during batch investigations was observed despite the elevated temperature (380 °C) and high RPM (1100) due to the high density difference compared to H2, especially in the case of CO2.

Introduction

The rapid growth of world’s population and rising desire for prosperity are driving the demand for energy and transportation fuels. According to the IEA scenarios [1, 2], this goes along with increasing importance of biofuels. To overcome limitations in blending potential of biofuels, drop-in quality is favourable. One established pathway in this direction is the production of hydroprocessed vegetable oil [3].

A comparable approach is a two-step upgrading of vegetable oils via thermal deoxygenation (DO) in the first step producing CVO and subsequent hydroprocessing to obtain hydroprocessed CVO [4, 5]. The CVO production step was investigated in detail before; during this step, a decrease of the vegetable oils’ initial oxygen content (approximately 10 wt %) to 5 wt % was reached [4, 6]. It was shown that the CVO’s oxygen is mainly (87 wt %) bound in free fatty acids [5]. Batch studies on HDO of CVO gave the first indications of catalytic influences on oxygen and energy content of hydroprocessed CVO [5]. Semi-continuous studies were performed to approach suitable feed rates (CVO, H2) for the continuous HDO of CVO [7]. Optimal reaction conditions for all investigations of this work were found to be 380 °C, 50 bar H2 pressure and a gas entrainment impeller rotation speed of 1100 RPM [5, 7].

DO and HDO of fatty acids is widely discussed in literature [815]. HDO implies the direct participation of H2 in a reaction, while DO in general does not necessarily require H2. According to the aforementioned literature, the main gaseous products from DO/HDO of fatty acids are CO2 from decarboxylation and CO from decarbonylation reactions for both DO and HDO, while reaction water may result from at least three pathways: first, along with decarbonylation; second, from dehydration (during DO/HDO) and third, via hydrogenation (reduction) in case of HDO. Further gaseous products may be short-chain hydrocarbons such as CH4 and C2H6. One possibility for the formation of hydrocarbon gases is cracking [8, 16]. CH4 can also result from GPRs such as methanation of CO and CO2. Furthermore, CO can also result from CO2 and H2 via RWGS. These GPRs as shown in Eqs. (13) are reported by Gusmão et al. [12], Wagman et al. [17], Snåre et al. [18], Lestari et al. [19] and Madsen et al. [11].

The present work focuses on three main questions: Which are the main gaseous and liquid products occurring during HDO of CVO? Which interrelationship between gas and liquid-phase composition can be identified? Which GPRs can take place in parallel of HDO of CVO? Based on these questions, the objective of this work is to study the influence of two different catalysts: A typical hydrotreatment catalyst CoMo/Al2O3 and Pt/C as a noble metal catalyst [20]. For the HDO investigations of CVO, continuous experiments are performed. GPRs are studied using a batch configuration of the setup to allow an overall mass balance of the experiments. Thermodynamics of GPRs are worked out to support the findings from the experimental work.

Thermodynamic section of GPRs

The thermodynamic section shall give some insights regarding Gibbs free energy and reaction equilibrium data for the considered GPRs. The main gaseous products observed during HDO of CVO are CO2, CO and CH4. According to the literature mentioned above, RWGS and methanation of CO and CO2 are the expected GPRs under H2 atmosphere (13).

$${\text{CO}}_{2} + {\text{H}}_{2} \mathop \leftrightarrow \limits^{{{\text{T}},{\text{p}}}} {\text{CO}} + {\text{H}}_{2} {\text{O,}}$$
(1)
$$\underline{{{\text{CO}} + 3{\text{H}}_{2} \mathop \leftrightarrow \limits^{{{\text{T}},{\text{p}}}} {\text{CH}}_{4} + {\text{H}}_{2} {\text{O,}}}}$$
(2)
$${\text{CO}}_{2} + 4{\text{H}}_{2} \mathop \leftrightarrow \limits^{{{\text{T}},{\text{p}}}} {\text{CH}}_{4} + 2{\text{H}}_{2} {\text{O}}.$$
(3)

Equation (3) may be represented by the combination of Eqs. (1) and (2). Therefore, reactions (1, 2) will be mainly considered in the following. To compare experimental results with thermodynamic equilibrium, data for reactions (1, 2) were calculated for the applied reaction temperature. First, it was proved if the GPRs are exergonic or endergonic (Eq. 4). The calculation of reaction enthalpy and reaction entropy according to (5, 6) is carried out with data from Basu [21] and National Institute of Standards and Technology [22].

$$\Delta G_{R} = \Delta H_{R} - T \times \Delta S_{R} ,$$
(4)
$$\Delta H_{R} \left( T \right) =\Delta H_{R} \left( {T_{0} } \right) + \mathop \sum \nolimits v_{i} \cdot\left[ {a_{i} \cdot\left( {T - T_{0} } \right) + \frac{{b_{i} }}{2}\cdot\left( {T^{2} - T_{0}^{2} } \right) + \frac{{c_{i} }}{3}\cdot\left( {T^{3} - T_{0}^{3} } \right) + \frac{{d_{i} }}{4}\cdot\left( {T^{4} - T_{0}^{4} } \right)} \right],$$
(5)
$$\Delta S_{R} \left( T \right) =\Delta S_{R} \left( {T_{0} } \right) + \mathop \sum \nolimits v_{i} \cdot\left[ {a_{i} \cdot{ \ln }\left( {\frac{T}{{T_{0} }}} \right) + b_{i} \cdot(T - T_{0} ) + \frac{{c_{i} }}{2}\cdot(T^{2} - T_{0}^{2} ) + \frac{{d_{i} }}{3}\cdot(T^{3} - T_{0}^{3} )} \right],$$
(6)

where \(\Delta G_{R}\) Gibbs free energy (kJ/mol), \(\Delta H_{R}\) reaction enthalpy (kJ/mol), \(T\) temperature (K), \(\Delta S_{R}\) reaction entropy (kJ/mol K), \(\Delta H_{R} (T_{0} )\) reaction enthalpy at T 0 (1 bar) using data from National Institute of Standards and Technology [22] (kJ/mol), \(T_{0}\) reference temperature (298.15 K) (K), \(v_{i}\) stoichiometric factor of component i, \(a_{i} \ldots d_{i}\) coefficients of component i according to Basu [21] (kJ/mol), \(\Delta S_{R} (T_{0} )\) reaction entropy at T 0 (1 bar) using data from National Institute of Standards and Technology [22] (kJ/mol K).

It was found that the RWGS is endergonic in the considered temperature range, whereas CO-methanation is exergonic, as can be seen from Gibbs free energy for each reaction. Detailed results are shown in Table 1.

Table 1 Calculated reaction enthalpy ΔΗ R , reaction entropy ΔS R and Gibbs free energy ΔG R for GPRs according to Eqs. (1, 2) depending on temperature at 1 bar

These values are in good agreement with the literature data from Snåre, et al. [18] which provided data for the reaction enthalpy and Gibbs free energy for reactions (1) and (2) at 573.15 K (ΔΗ R,(1) = 39.2 kJ/mol, ΔΗ R,(2) = −216.4 kJ/mol, ΔG R,(1) = 17.6 kJ/mol, ΔG R,(2) = −78.7 kJ/mol).

Due to these thermodynamic results, a low equilibrium constant (K p,(1)) is expected for RWGS, while equilibrium constant for CO-methanation should be high. The thermodynamic equilibrium constant for the RWGS reaction (1) and CO-methanation (2) are calculated according to Eq. (7) based on the data from Elvers [23].

$$K_{p} = 10^{{\left( {a + \frac{b}{T} + c\cdot\log \left( T \right) + d\cdot\;T + e\cdot\;T^{2} } \right)}} ,$$
(7)

where \(K_{p}\) equilibrium constant, \(a \ldots e\) coefficients according to Elvers [23], \(T\) temperature in K.

Accordingly, the equilibrium constants for RWGS (1) and CO-methanation (2) were calculated. Equilibrium constants are 0.070 for RWGS (1) and 6 × 104 bar−2 for CO-methanation (2) (at 380 °C, 1 bar).

Experimental section

Materials

Two different catalysts were used: molybdenum with cobalt traces on an Al2O3 support (CoMo/Al2O3; BET surface area = 140 m2/g; 20 wt % MoO3, 5 wt % CoO; 9.4 nm mean pore diameter; 0.34 mL/g pore volume) and platinum on a carbon support (Pt/C; BET surface area = 650 m2/g; 5 wt % Pt; 2.4 nm mean pore diameter; 0.39 mL/g pore volume). Both catalysts were provided by Clariant International, Ltd. (Muttenz, Switzerland). Calibration gases (N4, N21, Crystal-mixtures) and H2 (purity > 99.999 mol %) were purchased from Air Liquide (Hamburg, Germany). Pt and CoMo catalysts for HDO purposes were applied and have already been widely studied [5, 2428]. The CoMo catalyst was provided string-shaped in a basket, and the Pt catalyst as a fine powder. CVO was produced from rapeseed oil [4].

Methods

The experiments were all performed using an autoclave (type 4576A, Parr Instruments, Moline, IL, USA) at 380 °C, 50 bar H2 pressure and with the gas entrainment impeller running at 1100 RPM. In previous investigations, these process conditions were found to be optimal for the catalytic HDO of CVO [5, 7]. The piping and instrumentation diagram of the test plant is presented in Fig. 1.

Fig. 1
figure 1

Piping and instrumentation diagram of the test plant. Acronyms according to [29]: A alarm, C control, F flow, I indication, P pressure, R record, S speed, T temperature

11 experiments were performed in total (Table 2). The experiments included the following:

Table 2 Overview of the performed experiments (380 °C, 50 bar H2)
  • Continuous liquid-phase DO via catalytic HDO of CVO.

  • Continuous investigations of gas residence time behaviour of the test plant.

  • Batch experiments for the characterisation of GPRs.

  • Batch investigations of gas phase inhomogeneity.

For the continuous catalytic HDO of CVO, H2 and CVO were fed continuously into the process. The operation mode of the pilot plant is termed reactive stripping and was derived from the reactive distillation mode in the production process of CVO [4]. The reactor was mounted, rendered inert and finally CVO was provided in the reactor to give a filling level of two-thirds at the reaction temperature relative to the overall reactor volume. H2 acts as a stripping and hydrogenation gas. The H2 flow was set to 2.5 g/h by means of a mass flow counter (type M 12202139A, Bronkhorst High-Tech B.V., Ruurlo, Netherlands). Comparable investigations used a similar flow for H2 [13, 30]. The liquid feed rate was 3.5 g/h and was chosen according to the preliminary investigations in semi-continuous mode [7]. Condensate samples were released continuously every 30 min at the beginning and then every 60 min after approximately 3 h time on stream (condensate fraction). The sump fraction was collected in the reactor. The catalytic HDO of CVO was run continuously investigating time on stream between 7 and 12 h. The preparation of all continuous catalytic HDO experiments was identical to assure reproducibility.

Continuous discharge of gas (CO and CO2, CO x in the following) was calculated according to Eq. (8) based on measurement data of the nondispersive infrared photometer.

$$m_{{{\text{CO}}_{x} }} = \mathop \sum \limits_{j} \dot{V}_{{{\text{ges}},\Delta t,j}} \times \overline{{\rho_{{{\text{CO}}_{x} ,\Delta t,j}} }} \times (t_{j + 1} - t_{j} ) \times \frac{{\left( {v_{j} + v_{{{\text{j}} + 1}} } \right)}}{2}.$$
(8)

Volume fractions (\(v_{j} + v_{{{\text{j}} + 1}}\)) measured by a nondispersive infrared photometer in each time interval (\(t_{j + 1} - t_{j} )\), the total gas volume flow (\(\dot{V}_{{{\text{ges}},\Delta t,j}}\)) and density of CO x (\(\overline{{\rho_{{{\text{CO}}_{x} ,\Delta t,j}} }}\)) were required parameters for the calculation.

The molar ratio of decarbonylation/decarboxylation alkane products (dec) versus the hydrodeoxygenation alkane products (hyd) is calculated according to Eq. (9):

$$\frac{\text{dec}}{\text{hyd}} = \frac{{\mathop \sum \nolimits_{i}\Delta n_{{i,{\text{C}}_{n - 1} }} }}{{\mathop \sum \nolimits_{i}\Delta n_{{i,{\text{C}}_{n} }} }},$$
(9)

where \(\frac{\text{dec}}{\text{hyd}}\) molar ratio of produced C n - and C n−1-alkanes, \(\Delta n_{{i,{\text{C}}_{n - 1} }}\) net molar production of C n-1-alkanes (C8, C9, C15, C17) (mol), \(\Delta n_{{i,{\text{C}}_{n} }}\) net molar production of C n -alkanes (C9, C10, C16, C18) (mol).

The net molar production of the respective alkanes was taken from GC/MS/FID analysis. The selection for alkanes (C8, C9, C10, C15, C16, C17 and C18) is related to chain length of the respective main fatty acids (C9, C10, C16, C18) in the CVO. These four selected fatty acids were found in concentrations ≥ 1.5 wt % in CVO and decomposed totally during HDO. The decomposition of these fatty acids can result in unchanged chain length alkanes, so called C n -alkanes (C9, C10, C16, C18) via hydrogenation (reduction). The second possibility of decomposition is the chain length reduction by one carbon, resulting in the so-called C n−1-alkanes (C8, C9, C15 and C17) via decarbonylation and decarboxylation. The procedure of using molar product ratios for the characterisation of possible reactions was used in other studies before [13, 3133].

For the continuous gas residence time studies, the same constant flow of H2 was used as in continuous HDO experiments for the purpose of comparison (2.5 g/h). CO2 was injected for pulsed tagging, once the reaction temperature was reached by means of a Teledyne Isco high-pressure pump (type 500 HP, Lincoln, NE, USA) via the liquid feed inlet. Two setups were investigated: one without liquid filling the reactor and one with filling the reactor with an inert liquid medium (BP Energol CS-HB 220). The liquid level of the reactor was (according to the experiments for the catalytic HDO of CVO) two-thirds at the reaction temperature relative to the overall reactor volume. Regarding the gas residence time, the CO2 pulse passed the test plant (Fig. 1) in the same way as the reaction gases formed in an experiment for the catalytic HDO of CVO (experiment 1–5) as follows: it was injected in the reactor and passed the condenser and the settling vessel of the liquid samples before the gas concentration was measured by the nondispersive infrared photometer. For both experiments on the gas residence time, approximately the same amount of CO2 was injected. The mean gas residence time was calculated considering CO2 concentration over time using linear interpolation between the measurement points. The gas residence time investigations were performed without catalysts to avoid GPRs.

For the batch investigations of the catalyst’s selectivity for GPRs, the reactor was operated in batch mode. The procedure of preparation was the same as for a continuous HDO experiment, but without liquid filling. The catalyst amount was the same as for an experiment for the catalytic HDO of CVO (0.91 g for CoMo/Al2O3, 0.48 g for Pt/C, Table 3). After filling with H2, the reactor was heated to the reaction temperature (380 °C). The first sample of each experiment was taken before the CO2 injection to obtain a comparison value. Afterwards, the reactor pressure was adjusted to 50 bar H2, and CO2 was injected for pulsed tagging. The gas entrainment impeller was run at 1100 RPM. The experiments with both the catalysts were performed with similar initial concentration of CO2 to ensure the comparability of the results. Gas sampling intervals were 5 min after injection. Each sample was drawn directly from the reactor after cooling and expansion to ambient conditions. Six samples could be taken from the overall reactor volume. Samples were then prepared for the GC/FID analysis.

Table 3 Results of the continuous HDO experiments at 380 °C and 50 bar H2 performed with CVO and CoMo/Pt as catalysts

The inhomogeneity of the gas phase in the reactor was investigated in batch mode considering two different sampling locations, using the CO2 concentration as an indicator. The CO2 injection was performed once the reactor reached 380 °C. Sampling was performed approximately 5 min after the CO2 injection. The first sampling location was on the top of the reactor (approximately 86 mm from the bottom), and the second sample was drawn via the dip tube (approximately 25 mm from the bottom). Both samples were taken simultaneously.

Analysis of liquid and gaseous products

Liquid samples

For the liquid sample analysis, a G1530A GC (Agilent Technologies, Santa Clara, CA, USA) coupled with a quadrupole MS (5972A HP 6890, Hewlett Packard, Palo Alto, CA, USA) and FID was used. The database of the National Institute of Standard and Technology was used for the component identification. A VF5-ms capillary column from Agilent Technologies was installed (60 m × 0.25 mm × 0.25 µm). Perylene (C20H12) and used as an internal standard to avoid overlapping with component peaks. The split ratio was set to 15:1. The initial temperature of the column was 45 °C (holding time 4 min), followed by a heating ramp of 3 °C/min until 320 °C was reached. The final column temperature was held for 20 min. The GC was run in a constant flow mode with helium as the carrier gas at 2 mL/min. The average flow velocity was 31 cm/s. The FID was run at 350 °C. Nitrogen was used as the makeup gas with a flow of 45 mL/min; the synthetic air flow was 450 mL/min, and the H2 flow was 40 mL/min. MS and FID detector was used in tandem for best identification and quantification of the components. The process of sample preparation was reproducible. Linear fitted curves were used for the calculation of the quantity of each component in agreement with the procedure applied by Artigues et al. [34].

Continuous gas composition

A calibrated Infralyt 50 nondispersive infrared photometer (Saxon Corporation, Dessau-Roßlau, Germany) was used for the continuous gas analysis. The nondispersive infrared photometer was used for both the experiments of the catalytic HDO of CVO and the gas residence time investigations.

Batch gas samples

The compositions of the batch gas samples were quantified with GC/FID on an Agilent Technologies 6890 N (G1530 N) machine equipped with a CoraPlot Q capillary column (CP7554, 25 m length, 0.53 mm inner diameter and 20 µm film thickness). The split was set to 10:1. The carrier gas was helium, with a flow of 20 mL/min. The initial oven temperature was 50 °C. The first heating ramp was 20 °C/min until 95 °C was reached and held for 4 min. The final temperature was 100 °C, reached with a second heating ramp of 12 °C/min. The FID was run at 220 °C. The H2 flow was 40 mL/min, the air flow was 400 mL/min and the nitrogen makeup flow was 12 mL/min. The components were assigned according to their retention time similarity. Calibration runs with different test gases were performed as repeat determinations. Linear fitted curves were used to calculate the quantity of each component.

The gas samples were additionally analysed on a calibrated micro gas chromatograph (GCM Micro Box I, SLS Micro Technology Corporation, Mainz-Kastel, Germany) to confirm the gas composition results. A HayeSepA packed column was used for the measurement by means of a thermal conductivity detector. Argon was used as a carrier gas at a pressure of 3.5 bar.

Results and discussion

Results and discussion are given in two main chapters in the following order:

Continuous processing

  • Liquid-phase DO via catalytic HDO of CVO for upgrading raw material CVO and to identify possible reactions.

  • Gas residence time behaviour of the test plant.

Batch experiments

  • Characterisation of GPRs.

  • Inhomogeneity effect.

11 experiments were performed in total. An overview of these experiments is given in Table 2.

Continuous processing

The results of the HDO experiments as well as the gas residence time behaviour of the test plant are given in this chapter.

Liquid-phase DO via Catalytic HDO of CVO

Table 3 gives the overall mass balances and oxygen content of CVO and main products (sump fraction) for five experiments of the continuous catalytic HDO of CVO with 3.5 g/h feed and 2.5 g/h H2 mass flow. The rotational speed of the gas entrainment impeller was 1100 RPM.

As can be seen from Table 3, sump fraction is the main liquid product. This is due to the initial filling of the reactor with CVO. The highest DO of the sump fraction was observed with 12 h time on stream in experiment 5. The lowest oxygen concentration is confirmed by the highest mass of \(m_{{{\text{CO}}_{x} }}\) for experiment 5 within all experiments (1–5). The overall mass balance is rising from 85 to 95 wt % with an increase in time on stream if we compare the experiments 3, 4 and 5 with Pt/C catalyst.

The results of the gas phase composition (nondispersive infrared photometer) are shown in Figs. 2 and 3 for all five experiments. Starting at time zero (heating switched on), the heating period until reaching the target temperature (380 °C) was approximately 1 h (62–64 min).

Fig. 2
figure 2

Concentrations of CO and CO2 during HDO at 380 °C and 50 bar H2 with CoMo catalyst, A heating switched on, B heating switched off

Fig. 3
figure 3

Concentrations of CO and CO2 during time on stream for the HDO experiments at 380 °C and 50 bar H2 with Pt catalyst, A heating switched on, B heating switched off for experiment 3, C for experiment 4, D for experiment 5

CO was detected slightly before CO2 in every experiment. As the decrease in CO concentration in experiment 5 from 0.5 to 0.4 vol % took place very slowly (approximately within 5 h), it may be expected that the process was close to steady state at point C. It can be seen in Figs. 2 and 3 that the main DO of the liquid phase takes place rapidly at the beginning of the experiment due to steep inclination of the gas concentrations. Main product’s (sump fraction) oxygen content confirms high DO after time on stream with both the catalysts (Table 3). Possibly the CO and CO2 concentrations result from the DO/HDO reactions decarboxylation and decarbonylation. Considering this assumption, it can be seen that the Pt catalyst was more selective for these DO/HDO reactions compared to the CoMo catalyst. This is in agreement with literature, as can be seen in Table 4.

Table 4 Product ratios (dec/hyd) from different model compounds resulting from DO/HDO reactions under a H2 atmosphere using CoMo and Pt catalysts

A dec/hyd ratio of 1 indicates the presence of both decarbonylation/decarboxylation and hydrogenation to the same extent. This is the case for both experiments with the CoMo catalyst (experiment 1 and 2). The same dec/hyd ratios of these experiments confirm reproducibility. Pt catalysts give clearly higher dec/hyd ratios than CoMo catalysts using vegetable oils as feedstocks. This effect is still visible in the HDO of CVO in this work. The lower dec/hyd ratio for CVO compared to the other results with Pt catalyst is due to the strongly reduced oxygen content of the CVO [36, 37]. This means, that the main part of decarbonylation/decarboxylation already occurred in the previous CVO production step [4]. In general, higher CO x -yields should go along with increasing dec/hyd ratios. This is confirmed by the data of this work given in Table 4.

Due to the higher concentration of CO compared to CO2, both catalysts seem to be more selective for decarbonylation over decarboxylation. However, it is possible that the CO2 is continuously decomposed to CO via GPRs during the HDO of CVO as well. CH4 and C2H6 were measured only batch-wise every 30 min by micro gas chromatography. The maximum values for the CoMo catalyst (experiment 1) were 0.13 vol % for CH4 and C2H6, and for the Pt catalyst (experiment 3) 0.16 vol % for CH4 and 0.30 vol % for C2H6 were reached.

Due to the gas phase composition observed (mainly H2, CO and CO2), GPRs may occur (Eqs. 13). The gas concentrations (Figs. 23) are compared to gas residence time behaviour of the plant to identify reaction time of main DO/HDO.

Gas residence time behaviour of the test plant

The gas residence time behaviour of the plant was investigated with and without filling the reactor with an inert liquid medium. Two experiments (6, 7) were performed. CO2 pulsed tagging was applied for these investigations. Figure 4 shows the results of the CO2 concentration plotted over time measured via a nondispersive infrared photometer.

Fig. 4
figure 4

Gas residence time behaviour of the test plant at 380 °C and 50 bar H2 (1100 RPM, 2.5 \({\text{g}}_{{{\text{H}}_{2} }} /{\text{h}}\))

Mean gas residence time for experiment 6 (B) and for experiment 7 (C) is shown. Downtime (A) of both the experiments was 26 min. As can be seen in Fig. 4, the downtime of both experiments was 26 min. It is defined as the time period between the pulse injection and the first detection of the gas by the nondispersive infrared photometer. Taking the downtime into account, the starting time of the DO during the catalytic HDO of CVO (experiments 1–5) is approximately 26 min before the first detection of CO. This result highlights the importance of downtime/residence time characteristics to be considered; especially for the discussion of reaction temperature in conjunction with reaction time. The steep inclination of the CO2 concentrations is in agreement with the gas concentrations observed during HDO of CVO (Figs. 23). This confirms the fast DO/HDO of the main liquid product at the beginning of a HDO experiment (1–5). Regarding Figs. 2 and 3, the first detection of CO is close to the time needed to reach the target temperature of 380 °C. Taking downtime into account, this means that the formation of CO begins approximately 26 min earlier during the heating period. As a result, this indicates for experiments 1–5 that the starting temperature for DO/HDO via CO release is ≥230 °C. The formation of CO2 began at approximately 365–375 °C in all five experiments (1–5). Successful HDO with Pt/C at a similar temperature (250 °C) was reported elsewhere [20]. Partly HDO of rapeseed oil with CoMO catalyst at 200 °C was reported from Pinto et al. [38]. HDO processes in this temperature range (≤250 °C) are often called mild HDO [20, 39].

Experiment 7, with an inert liquid filling, showed a higher maximum CO2 concentration but the same downtime as experiment 6, without liquid filling. This may be due to both a higher concentration of CO2, caused by the smaller gas volume in the reactor due to the liquid filling and the higher amount of injected CO2, caused by the limited setting accuracy of the high-pressure pump. According to Fig. 4, the injected quantity of CO2 and/or the filling of the reactor with an inert liquid media influenced the mean gas residence time slightly. Mean gas residence time was evaluated by linear interpolation between the measurement points. The mean gas residence time was 42 min for experiment 6 and 45 min for experiment 7.

Batch experiments

Characterisation of gas phase reactions

GPRs (1–3) may be responsible for the rapidly decreasing CO2 concentration in the gas phase (Figs. 23). For this reason, the selectivity of these chemical reactions was investigated with both the catalysts in experiments 8 and 9. After the CO2 injection, six gas samples were taken from the reactor in each experiment (Fig. 1). The development of the reactor pressure during sampling in experiments 8 and 9 is shown in Fig. 5.

Fig. 5
figure 5

Development of inner reactor pressure during the investigation of the GPRs without liquid filling at 380 °C, 50 bar. Experiment 8: CoMo catalyst, experiment 9: Pt catalyst

As can be seen in Fig. 5, the reactor pressure was constant between each gas sampling in the experiment with the CoMo catalyst (experiment 8), but it increased in the experiment with the Pt catalyst. It is assumed that this finding is due to the adsorption/desorption effects on the support of the catalyst (active carbon). Each stage in the diagram indicates a gas sample. Gas samples were removed until the reactor was evacuated. The adsorption/desorption of H2 on Pt catalyst on active carbon (5 wt % Pt, BET = 650 m2/g) was observed as well by Wang and Yang [40] (6 wt % Pt, BET = 3126 m2/g). These authors showed a higher adsorption capacity of metal-doped carbon than that of plain carbon. At 50 bar and 298 K, the amount of H2 adsorbed on Pt/carbon was found to be approximately 0.75 wt %, related to the mass of the catalyst [40]. The adsorbed amount depends on the reaction time, temperature and BET surface area.

Results from GC/FID analysis of the gas sample composition in experiments 8 and 9 are shown in Figs. 6 and 7.

Fig. 6
figure 6

CO and CO2 concentration from experiment 8 (CoMo) and experiment 9 (Pt) at 380 °C and 50 bar. Sample time: 5 min after CO2 injection at time zero (then 5 min intervals)

Fig. 7
figure 7

CH4 concentration in the gas samples of experiment 8 (CoMo) and experiment 9 (Pt) at 380 °C and 50 bar

Experiments 8 and 9 showed a remarkable CO2 gas phase conversion due to CO and CH4 generation. CO2 conversion was obviously supported to a higher extend with the Pt catalyst compared to the CoMo catalyst. The detection of CO was unexpected, as the equilibrium constant for the CO-methanation reaction (2) according to Eq. (7) is 6 × 104 bar−2, indicating the complete reaction of CO to CH4. A possible explanation is the kinetic inhibition of the CO-methanation (2). A further unexpected observation in Fig. 7 is the initial concentration of CH4 above zero (0.22 vol %) prior to the injection of CO2. A reason could be that the CH4 was generated by Pt supported reaction of the active carbon carrier material and the H2 atmosphere during the heating phase (approximately 50 min).

Based on the results shown in Figs. 6 and 7, the quantity of each component was calculated according to ideal gas law, and the results are summarised in Table 5.

Table 5 Quantity of each component from experiments 8 and 9 based on ideal gas law calculations

Higher hydrocarbons were not considered due to their very low concentrations (≤0.11 vol %) during the entire experiments. The total carbon discharge in the collected gas samples was used to calculate the initial concentration of the CO2 in the reactor, as given in Table 5 and marked on the ordinate in Fig. 6. In the two experiments, the injected quantity of CO2 was nearly the same. The experimental procedure was reproducible and the initial CO2 concentrations were comparable in both experiments (8 and 9).

With these experimental data and the equilibrium constant calculated before the theoretical maximum partial pressure of CO (p CO) at RWGS’s equilibrium without subsequent methanation was calculated according to Eq. (10).

$$K_{p,(1)} = \frac{{p_{\text{CO}} \cdot p_{{{\text{H}}_{2} {\text{O}}}} }}{{p_{{{\text{CO}}_{2} }} \cdot p_{{{\text{H}}_{2} }} }} = \frac{{p_{\text{CO}}^{2} }}{{\left( {p_{{0,{\text{CO}}_{2} }} - p_{\text{CO}} } \right)\cdot p_{{{\text{H}}_{2} }} }},$$
(10)

where \(K_{p,(1)}\) equilibrium constant for RWGS (1), \(p_{\text{CO}}\) equilibrium partial pressure CO (bar), \(p_{{{\text{H}}_{2} {\text{O}}}}\) equilibrium partial pressure H2O (bar), \(p_{{{\text{CO}}_{2} }}\) equilibrium partial pressure CO2 (bar), \(p_{{{\text{H}}_{2} }}\) equilibrium partial pressure H2 (bar), \(p_{{0,{\text{CO}}_{2} }}\) initial partial pressure CO2 (bar).

Disregarding subsequent reactions of CO, partial pressures for equilibrium of RWGS were defined as follows: \(p_{\text{CO}} = p_{{{\text{H}}_{2} {\text{O}}}}\) and \(p_{{{\text{CO}}_{2} }} = p_{{0,{\text{CO}}_{2} }} - p_{\text{CO}}\).

The initial partial pressure of \({\text{CO}}_{2} \left( {p_{{0,{\text{CO}}_{2} }} } \right)\) in Eq. (10) was calculated from the total initial reactor pressure multiplied by the experimental initial CO2 concentration, as given in Table 5. The equilibrium partial pressure of \({\text{H}}_{2} \left( {p_{{{\text{H}}_{2} }} } \right)\) was set equal to the difference between the measured initial reactor pressure after injection of CO2 and the calculated \(p_{{0,{\text{CO}}_{2} }}\) by approximation. Based on these preconditions, the equilibrium partial pressure of CO (p CO) was calculated from Eq. (10). Results are given in Table 6.

Table 6 Theoretical maximum partial pressure of CO based on equilibrium of Eq. (1) calculated from Eq. (10)

The results from Table 6 show that \(p_{{{\text{CO}}_{2} }}\) must be lower at RWGS’s equilibrium compared to p CO. Based on the data from Table 6 theoretical maximum yields of CO/H2O from RWGS at equilibrium can be calculated via p CO and ideal gas law, as one mole of CO results in one mole of H2O: \(n_{\text{CO}} = n_{{{\text{H}}_{2} {\text{O}}}} = p_{\text{CO}} \cdot\;V_{\text{Reactor}} /R\cdot\;T_{\text{Reactor}}\). By molar mass (\(m_{{{\text{H}}_{2} {\text{O}}}} = n_{{{\text{H}}_{2} {\text{O}}}} /M_{{{\text{H}}_{2} {\text{O}}}}\)), H2O yields were calculated. The theoretical maximum yields of CO and H2O are given in Table 7.

Table 7 Theoretical maximum yields of CO and H2O based on equilibrium of RWGS (1)

The experimental CO-yields of experiments 8 and 9 according to Table 6 are approximately 50 % below the theoretical maximum yields as shown in Table 7 and therefore within the expected theoretical limits. Presuming RWGS to occur, the formation of H2O occurs in the same quantity compared to CO. The calculation of the H2O-yields based on the experimental CO-yields for experiment 8 and 9 gave the following results:

  • Experiment 8: \(m_{{{\text{H}}_{2} {\text{O}}}}\)  = 0.06 g H2O (\(M_{{{\text{H}}_{2} {\text{O}}}}\) · 0.0033 molCO).

  • Experiment 9: \(m_{{{\text{H}}_{2} {\text{O}}}}\)  = 0.11 g H2O (\(M_{{{\text{H}}_{2} {\text{O}}}}\) · 0.0061 molCO).

These low mass yields of H2O could not be detected. They probably disappeared by condensation in the gas samples. As expected, the theoretical maximum yields of H2O were found to be higher than the calculated yields based on measurements. This can be seen when comparing the values from the experiments (8, 9) to the values given in Table 7.

Inhomogeneity effect

During the experimental investigations of the GPRs, an inhomogeneity of the gas phase was observed in the reactor. The first indicators could be detected in experiments 8 and 9, and the phenomenon is proven in experiments 10 and 11. This inhomogeneity effect made further kinetic investigations of GPRs impossible. However, the balance of the detected gas components could be analysed (Table 5).

The steady increase of CO and CO2 shown in Fig. 6 gives the first indication of this inhomogeneity, which was caused due to density differences of the gases compared to H2 (CO and CO2 by factors 22 and 14, respectively). In the first gas sample, H2 was predominantly removed, but in the last sample, the CO and CO2 could expand more in the reactor, thus gradually raising the local concentration at the measuring point for each sample. The indication of inhomogeneity in experiments 8 and 9 can be derived from the fact that the measured CO2 concentrations in the gas samples exceed the initial CO2 concentration at the end of each investigation (Fig. 6), despite the CO2 decomposition. Remarkably, this inhomogeneity effect occurred even though the gas entrainment impeller was run at 1100 RPM and the reactor temperature was 380 °C.

The measuring points for the gas samples are indicated in Fig. 8 in a simplified true-scale drawing (experiments 8 and 9: sample dip tube, experiments 10 and 11: sample dip tube and on the top of the reactor).

Fig. 8
figure 8

True to scale drawing of the reactor interior; overall height approx. 86 mm, gas entrainment impeller and dip tubes for sampling

For the practical validation of the inhomogeneity effect, experiments 10 and 11 were carried out without catalyst and liquid filling in the reactor, considering the two different measuring points in the reactor. The CO2 concentrations of the samples were analysed via micro gas chromatography, and the results are given in Fig. 9.

Fig. 9
figure 9

CO2 concentration at 380 °C and 50 bar in H2 atmosphere in the reactor, comparing two measuring points [top of the reactor (black bar), sample dip tube (grey bar)]

Sampling was performed 5 min after the CO2 injection in both experiments 10 and 11 (sample 1) as before (in experiment 8 and 9). Sample 2 in experiment 11 was drawn immediately after sample 1. The quantitative reproducibility is limited (comparing experiment 10 and experiment 11, sample 1), but the inhomogeneity effect is obvious in all samples: The CO2 concentration is higher at the dip tube measuring point, close to the bottom of the reactor, despite simultaneous sampling. The increase in the CO2 concentration with the decreasing reactor pressure (comparing experiment 11, sample 1 and sample 2) is due to the expansion of the heavy gas phase.

Conclusions

Continuous experiments for the HDO of CVO were performed using an autoclave in a reactive stripping process. Used catalysts (Pt, CoMo) were suitable for this process due to high DO of the main product (sump fraction, Table 3). The main reaction gases were found to be CO2 and CO, while the latter showed a higher concentration. Dec/hyd ratios were determined based on liquid phase composition. These calculated ratios correlate with the CO x -yields calculated from the gas phase composition. The selectivity for DO/HDO via decarboxylation/decarbonylation is indicated by the dec/hyd ratio and was higher with the Pt catalyst compared to the CoMo catalyst.

To investigate whether the RWGS reaction (1) occurs, batch experiments for GPRs (CO2 + H2) were performed without CVO, using the same catalysts as in the continuous HDO experiments (CoMo, Pt). In these batch experiments, CO was found to be a product gas, indicating that the RWGS reaction occurs under the applied experimental conditions (380 °C, ca. 50 bar H2 and ca. 2 bar CO2). Additionally, CH4 was found, indicating that methanation (2–3) occurs as well.

Thermodynamic data showed that RWGS is endergonic and CO-methanation is strongly exergonic under the applied conditions. Due to that, low RWGS yields and high CO-methanation yields are expected. Nevertheless, calculated RWGS yields based on equilibrium were found to be still significant due to H2 excess. This was confirmed by GPR investigations with both catalysts. The experimental determined CO-yields were found to be within the theoretical limit. However, CO-methanation yields were found to be much lower than the expected according to low CH4-concentrations from GPR investigations. This indicates kinetic inhibition. Further kinetic evaluations of RWGS and CO-methanation reactions (12) were not possible due to an unexpected inhomogeneity of the gas component concentrations in the reactor.

The enrichment in CO2 and CO at the bottom of the reactor was clearly caused by the high density differences of the gas components CO2, CO and CH4 compared to H2 (factors 22, 14 and 8, respectively), despite the elevated temperature and high RPM (380 °C, 1100 RPM).

Such inhomogeneity found in a common type reactor widely applied in research may cause similar problems in comparable investigations of other research groups. Nevertheless, this issue was not observed in the considered literature. CFD tools are to be applied as a tool for further clarification of this issue and to allow the confirmation of the unexpected experimental results shown in the present investigation.

Abbreviations

HDO:

Hydrodeoxygenation

CVO:

Cracked vegetable oil

CoMo:

Cobalt molybdenum

Pt:

Platinum

GPRs:

Gas phase reactions

RWGS:

Reverse water–gas shift reaction

DO:

Deoxygenation

DEC:

Decarboxylation/decarbonylation

HYD:

Hydrogenation

References

  1. 1.

    International Energy Agency: World Energy Outlook 2012. FRA, Paris (2012)

    Google Scholar 

  2. 2.

    International Energy Agency World Energy Outlook: Executive Summary. FRA, Paris (2014). 2014

    Google Scholar 

  3. 3.

    Aatola, H., Larmi, M., Sarjovaara, T., Mikkonen, S.: Hydrotreated vegetable oil (HVO) as a renewable diesel fuel: trade-off between NOx, particulate emission, and fuel consumption of a heavy duty engine. SAE Int. J. Engines 1(1), 1251–1262 (2009)

    Article  Google Scholar 

  4. 4.

    Augustin, C., Willner, T.: Investigation of vegetable oil conversion by thermal deoxygenation and cracking for alternative biofuel generation. In: Leal Filho, W., Mannke, F., Mohee, R., Schulte, V., Surroop, D. (eds.) Climate-Smart Technologies, pp. 563–576. Springer, Berlin (2013)

    Chapter  Google Scholar 

  5. 5.

    Sievers, A.: Hydroprocessing of cracked vegetable oil. Ph.D. thesis, University of the West of Scotland, Paisley, GB (2013)

  6. 6.

    Augustin, C.: Das Verhalten von Pflanzenölen bei der thermischen Zersetzung und der Desoxygenierung zu regenerativen Energieträgern. Dissertation, Helmut-Schmidt-Universität/Universität der Bundeswehr Hamburg, Hamburg, DE, Hamburg (2016)

  7. 7.

    Baldauf, E., Sievers, A., Willner, T.: In New developments in hydroprocessing of cracked vegetable oil. In: Hoffmann, C., Baxter, D., Maniatis, K., Grassi, A., Helm, P. (eds.) European Biomass Conference and Exhibition, 23–26 June 2014, ETA-Florence Renewable Energies, pp. 1034–1037 (2014)

  8. 8.

    Gosselink, R.W., Hollak, S.A.W., Chang, S.-W., van Haveren, J., de Jong, K.P., Bitter, J.H., van Es, D.S.: Reaction pathways for the deoxygenation of vegetable oils and related model compounds. ChemSusChem 6, 1576–1594 (2013)

    Article  Google Scholar 

  9. 9.

    Jęczmionek, Ł., Porzycka-Semczuk, K.: Hydrodeoxygenation, decarboxylation and decarbonylation reactions while co-processing vegetable oils over NiMo hydrotreatment catalyst. Part II: thermal effects—experimental results. Fuel 128, 296–301 (2014)

    Article  Google Scholar 

  10. 10.

    Chang, C.-C., Wan, S.-W.: China’s motor fuels from tung oil. Ind. Eng. Chem. 39, 1543–1548 (1947)

    Article  Google Scholar 

  11. 11.

    Madsen, A.T., Rozmysłowicz, B., Simakova, I.L., Kilpiö, T., Leino, A.-R., Kordás, K., Eränen, K., Mäki-Arvela, P., Murzin, D.Y.: Step changes and deactivation behavior in the continuous decarboxylation of stearic acid. Ind. Eng. Chem. Res. 50(19), 11049–11058 (2011)

    Article  Google Scholar 

  12. 12.

    Gusmão, A., Brodzki, D., Djéga-Mariadassou, G., Frety, R.: Utilization of vegetable oils as an alternative source for diesel-type fuel: hydrocracking on reduced Ni/SiO2 and Sulphided Ni-Mo/γ-Al2O3. Catal. Today 5, 533–544 (1989)

    Article  Google Scholar 

  13. 13.

    Endisch, M., Kuchling, T., Roscher, J.: Process balances of vegetable oil hydrogenation and coprocessing investigations with middle-distillates. Energy Fuels 27, 2628–2636 (2013)

    Article  Google Scholar 

  14. 14.

    Jęczmionek, Ł., Porzycka-Semczuk, K.: Hydrodeoxygenation, decarboxylation and decarbonylation reactions while co-processing vegetable oils over a NiMo hydrotreatment catalyst. Part I: thermal effects—theoretical considerations. Fuel 131, 1–5 (2014)

    Article  Google Scholar 

  15. 15.

    Snåre, M., Mäki-Arvela, P., Simakova, I., Myllyoja, J., Murzin, D.: Overview of catalytic methods for production of next generation biodiesel from natural oils and fats. Russ. J. Phys. Chem. B 3(7), 1035–1043 (2009)

    Article  Google Scholar 

  16. 16.

    Kubátová, A., Luo, Y., Šťávová, J., Sadrameli, S.M., Aulich, T., Kozliak, E., Seames, W.: New path in the thermal cracking of triacylglycerols (canola and soybean oil). Fuel 90(8), 2598–2608 (2011)

    Article  Google Scholar 

  17. 17.

    Wagman, D.D., Kilpatrick, J.E., Taylor, W.J., Pitzer, K.S., Rossini, F.D.: Heats free energies, and equilibrium constants of some reactions Involving O2, H2, H2O, C, CO, CO2, and CH4. J. Res. Natl. Bur. Stand. 34, 143–161 (1945)

    Article  Google Scholar 

  18. 18.

    Snåre, M., Kubičková, I., Mäki-Arvela, P., Eränen, K., Murzin, D.Y.: Heterogeneous catalytic deoxygenation of stearic acid for production of biodiesel. Ind. Eng. Chem. Res. 45(16), 5708–5715 (2006)

    Article  Google Scholar 

  19. 19.

    Lestari, S., Mäki-Arvela, P., Beltramini, J., Lu, G.Q.M., Murzin, D.Y.: Transforming triglycerides and fatty acids into biofuels. ChemSusChem 2, 1109–1119 (2009)

    Article  Google Scholar 

  20. 20.

    Wildschut, J., Mahfud, F.H., Venderbosch, R.H., Heeres, H.J.: Hydrotreatment of fast pyrolysis oil using heterogeneous noble-metal catalysts. Ind. Eng. Chem. Res. 48(23), 10324–10334 (2009)

    Article  Google Scholar 

  21. 21.

    Basu, P.: Combustion and Gasification in Fluidized Beds, p. 473. Taylor & Francis, Boca Raton (2006)

    Book  Google Scholar 

  22. 22.

    National Institute of Standards and Technology Thermodynamische Daten. http://webbook.nist.gov/chemistry/. Accessed 28 Aug 2015

  23. 23.

    Elvers, B.: Formamides and hexamethylenediamine. In: Elvers, B., Hawkins, S., Ravenscroft, M., Rounsaville, J.F., Schulz, G. (eds.) Ullmann’s Encyclopedia of Industrial Chemistry, vol. A12, p. 632. Wiley-VCH, Weinheim (1989)

    Google Scholar 

  24. 24.

    Fisk, C.A., Morgan, T., Ji, Y., Crocker, M., Crofcheck, C., Lewis, S.A.: Bio-oil upgrading over platinum catalysts using in situ generated hydrogen. Appl. Catal. A 358(2), 150–156 (2009)

    Article  Google Scholar 

  25. 25.

    Şenol, Oİ., Viljava, T.R., Krause, A.O.I.: Hydrodeoxygenation of methyl esters on sulphided NiMo/γ-Al2O3 and CoMo/γ-Al2O3 catalysts. Catal. Today 100(3–4), 331–335 (2005)

    Google Scholar 

  26. 26.

    Cugini, A.V., Rothenberger, K.S., Ciocco, M.V., Veloski, G.V.: Comparison of hydrogenation and dehydrogenation behavior and coal conversion activity upon the addition of coal for supported and unsupported molybdenum catalysts. Energy Fuels 11, 213–220 (1997)

    Article  Google Scholar 

  27. 27.

    Iida, H., Itoh, D., Minowa, S., Yanagisawa, A., Igarashi, A.: Hydrogenation of soybean oil over various platinum catalysts: effects of support materials on trans fatty acid levels. Catal. Commun. 62, 1–5 (2015)

    Article  Google Scholar 

  28. 28.

    Hara, Y., Endou, K.: The drastic effect of platinum on carbon-supported ruthenium-tin catalysts used for hydrogenation reactions of carboxylic acids. Appl. Catal. A 239, 181–195 (2003)

    Article  Google Scholar 

  29. 29.

    DIN EN 62424, Darstellung von Aufgaben der Prozessleittechnik—Fließbilder und Datenaustausch zwischen EDV-Werkzeugen zur Fließbilderstellung und CAE-Systemen. In: (IEC 65/544/CDV:2013). Beuth, Berlin, pp. 1–107 (2014)

  30. 30.

    Wang, C., Liu, Q., Song, J., Li, W., Li, P., Xu, R., Ma, H., Tian, Z.: High quality diesel-range alkanes production via a single-step hydrotreatment. Catal. Today 234, 153–160 (2014)

    Article  Google Scholar 

  31. 31.

    Krár, M., Kovács, S., Kalló, D., Hancsók, J.: Fuel purpose hydrotreating of sunflower oil on CoMo/Al2O3 catalyst. Bioresour. Technol. 101(23), 9287–9293 (2010)

    Article  Google Scholar 

  32. 32.

    Kim, S.K., Brand, S., Lee, H.-S., Kim, Y., Kim, J.: Production of renewable diesel by hydrotreatment of soybean oil: effect of reaction parameters. Chem. Eng. J. 228, 114–123 (2013)

    Article  Google Scholar 

  33. 33.

    Kubička, D., Bejblová, M., Vlk, J.: Conversion of vegetable oils into hydrocarbons over CoMo/MCM-41 catalysts. Top. Catal. 53, 168–178 (2010)

    Article  Google Scholar 

  34. 34.

    Artigues, A., Puy, N., Bartrolí, J., Fábregas, E.: Comparative assessment of internal standards for quantitative analysis of bio-oil compounds by gas chromatography/mass spectrometry using statistical criteria. Energy Fuels 28(6), 3908–3915 (2014)

    Article  Google Scholar 

  35. 35.

    Kubička, D., Šimáček, P., Žilková, N.: Transformation of vegetable oils into hydrocarbons over mesoporous-alumina-supported CoMo catalysts. Top. Catal. 52(1–2), 161–168 (2009)

    Article  Google Scholar 

  36. 36.

    Gong, S., Shinozaki, A., Shi, M., Qian, E.W.: Hydrotreating of jatropha oil over alumina based catalysts. Energy Fuels 26(4), 2394–2399 (2012)

    Article  Google Scholar 

  37. 37.

    Madsen, A.T., Ahmed, E.H., Christensen, C.H., Fehrmann, R., Riisager, A.: Hydrodeoxygenation of waste fat for diesel production: study on model feed with Pt/alumina catalyst. Fuel 90(11), 3433–3438 (2011)

    Article  Google Scholar 

  38. 38.

    Pinto, F., Martins, S., Gonçalves, M., Costa, P., Gulyurtlu, I., Alves, A., Mendes, B.: Hydrogenation of rapeseed oil for production of liquid bio-chemicals. Appl. Energy 102, 272–282 (2013)

    Article  Google Scholar 

  39. 39.

    Boscagli, C., Raffelt, K., Zevaco, T.A., Olbrich, W., Otto, T.N., Sauer, J., Grunwaldt, J.-D.: Mild hydrotreatment of the light fraction of fast-pyrolysis oil produced from straw over nickel-based catalysts. Biomass Bioenergy 83, 525–538 (2015)

    Article  Google Scholar 

  40. 40.

    Wang, L., Yang, R.T.: Hydrogen storage properties of carbons doped with ruthenium, platinum, and nickel nanoparticles. J. Phys. Chem. 112, 12486–12494 (2008)

    Google Scholar 

Download references

Acknowledgments

The present work is supported by a scholarship of the Hanns-Seidel-Stiftung by funds from the Federal Ministry of Education and Research, Germany. GC/MS/FID analyses were performed at the Thünen Institute of Wood Technology and Wood Biology, Hamburg, Germany.

Author contributions

The manuscript was written through contributions of all authors. All authors have given approval to the final version of the manuscript and contributed equally.

Author information

Affiliations

Authors

Corresponding author

Correspondence to Emanuel Baldauf.

Ethics declarations

Conflict of interest

The authors declare that they have no conflict of interest.

Rights and permissions

Open Access This article is 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, provided you give appropriate credit to the original author(s) and the source, provide a link to the Creative Commons license, and indicate if changes were made.

Reprints and Permissions

About this article

Verify currency and authenticity via CrossMark

Cite this article

Baldauf, E., Sievers, A. & Willner, T. Hydrodeoxygenation of cracked vegetable oil using CoMo/Al2O3 and Pt/C catalysts. Int J Energy Environ Eng 7, 273–287 (2016). https://doi.org/10.1007/s40095-016-0214-4

Download citation

  • Received:

  • Accepted:

  • Published:

  • Issue Date:

  • DOI: https://doi.org/10.1007/s40095-016-0214-4

Keywords

  • Catalytic hydrodeoxygenation
  • Cracked vegetable oil
  • Biofuel
  • Gas residence time
  • Gas phase reactions
  • Gas phase inhomogeneity