The system incorporates three key components, the Quax 8S Node, G Node, and S Node, each designed for specialised data collection. The Quax 8S Node gathers voyage-specific data, including ship speed, longitude, and other navigational metrics. The Quax G Node focuses on the main and auxiliary engines, collecting critical performance data such as turbocharger RPM and power output. Meanwhile, the Quax S Node captures flow and RPM data, enhancing the system’s comprehensive monitoring capabilities.
Data collection was conducted between 1 February 2021, and 10 February 2023, yielding 1,064,161 data points recorded at one-minute intervals. After preprocessing, the dataset comprises 1,003,490 data points, representing approximately 1.96 years of continuous operation. The collected parameters include power, fuel flow, temperature, and density for generators, electrical load analysis of ship consumers, main engine exhaust, power output, load, speed, and fuel properties. Data on fuel cells, battery performance curves, converter voltage, and conversion efficiencies have been sourced from relevant literature and commercially available manuals for hybrid systems.
Figure 2 illustrates a sample of the collected data, showcasing the power outputs of the diesel generators (D/Gs).
After data collection, the sensory data, collected at one-minute intervals, were pre-processed. Removal of empty values and grid power calculation have been conducted. The formation of scenarios, including FCs, batteries, and WHRS, has been arranged. The hybrid grid simulation has calculated the total fuel consumption of the marine power distribution plant units. The EEXI, CII, and operational and upstream emissions have been computed after the fuel consumption calculation. A cost-benefit analysis has been performed by computing installation and fuel costs. Finally, an MCDM analysis using the Technique for Order of Preference by Similarity to the Ideal Solution (TOPSIS) has been conducted to determine the preferred configuration, including the system design’s size, environmental performance, and economic efficiency.
2.1. Case Study Description
The case study vessel is a Kamsarmax bulk carrier owned and managed by the project partner LASKARIDIS SHIPPING CO., LTD (based in Athens, Greece).
Table 1 illustrates the ship particulars.
The conventional marine power distribution system comprises three D/Gs working in parallel. The vessel’s electricity demand dictates the generated power, while its magnitude allows for flexibility in selecting the number of simultaneous D/Gs in operation, which is integral to the optimisation process [
45].
Figure 3 illustrates the simplified system scheme of the conventional system and the assessed hybrid power distribution systems.
The study separately evaluated the implementation of various FCs (i.e., SOFC, PEMFC, and PAFC), batteries, and WHRS. Their suitability, sizing, and usage scenarios were analysed based on environmental impact, economic feasibility, volume, weight, and availability for maritime applications. The utilisation of the D/G and its power capacity share was analysed across various scenarios involving FC/Battery/WHRS combinations, considering the vessel’s entire electrical demand and partial load sharing between the D/G and alternative systems. The waste heat sources for the WHRS were the exhaust gases from the M/E following the exhaust gas boiler. The battery system was modelled, with optimal charging and discharging voltages determined using a grid search algorithm that accounted for the state of charge (SoC), state of health (SoH), capacity, and voltage drop.
Table 2 presents the system configurations for load-sharing scenarios involving marine diesel engines (MDEs) and various (FC) types, along with the corresponding equipment weights and volumes.
The FCs utilised in this study, as shown in
Table 2, are all commercially available products widely applied in various industrial settings. SOFCs and PAFCs have been selected for suitability in marine applications due to their resilience to impurities in H
2. SOFCs have been assumed to operate on H
2, targeting ambitious decarbonisation goals for the future, while PAFCs have been evaluated with LNG to assess their feasibility for earlier implementation.
MCFCs, although highly suitable for marine propulsion applications [
46], have been excluded from this study due to their large-scale power outputs starting at 1.4 MW and significant spatial requirements, which are unsuitable for the electrification plant in the case study vessel. PEMFCs, on the other hand, are noted for their high power density and rapid start-up times. However, their sensitivity to H
2 purity poses a limitation. Despite this, PEMFCs are emerging as commercially viable solutions for marine applications, making them the third product in the analysis.
Alkaline fuel cells (AFCs) also offer good power density, albeit lower than PEMFCs, and share similar disadvantages regarding H
2 purity. Consequently, recent marine applications have prioritised PEMFCs over AFCs [
46], a rationale also reflected in this study. Additionally, AFCs have been excluded due to the lack of a robust dataset on commercially available products.
The determination of FC and Battery capacities is based on achieving equivalence to one or two D/Gs, depending on the available waste heat power. Hybrid 1 and 3 configurations have FC/Battery capacities adjusted to meet one D/G’s power, while Hybrid 2 and 4 systems correspond to two D/Gs. WHRS supports Hybrid 3 and 4 configurations, whereas Hybrid 1 and 2 do not. This approach ensures that the D/Gs are not operating at very low loads, which is considered in the design process by analysing the load data.
In
Table 2, the weights and volumes of PEMFCs are remarkably lower than solely D/Gs and configurations of D/Gs and other types of FCs. Since the fuel-reforming modules of the FCs are integrated with the rest of the system, SOFC and PAFC weigh more and occupy more space. On the other hand, the H
2 production system for PEMFC must be implemented externally for the examined product.
In Hybrid 1 and Hybrid 3 configurations, the FC/Battery system has been designed to meet the power of one D/G. On the other hand, Hybrid 2 and Hybrid 4 FC/Battery configurations have replaced two D/Gs.
Table 3 demonstrates the technical specifications of the D/Gs on the case study ship.
Table 3 shows the conventional marine diesel engine on the case study vessel.
Figure 4 illustrates its specific fuel consumption (SFC) and power curves with varying engine loads.
Regarding fuel requirement, SFC refers to the fuel consumed per unit of time necessary to generate a specified engine output [
47]. Curves presented in
Figure 4 have been utilised to calculate the fuel consumption of a conventional MDE operating HFO. The variable load of the D/Gs has been determined through simulation, and the corresponding SFC and power values were interpolated from the curve.
Two different fuel configurations have been evaluated for the FC setups. The PAFC system includes an integrated steam methane reformer to produce H
2 by reforming LNG. The SOFC system can operate with an integrated LNG decomposer or pure H
2 from another source. The H
2 bunkering scenario has been assessed exclusively for SOFCs. PEMFCs require high-purity H
2, and its supply from an external facility has been considered in this study. For volume calculations, the dimensions of the SOFC reformer system were used.
Table 4 depicts the technical specifications of the assessed FC models.
The power values for each FC are provided for a single module. While PEMFC operates exclusively on highly purified H
2, SOFC and PAFC can also utilise LNG, resulting in significantly larger module sizes than PEMFC. PAFCs incorporate an integrated H
2 production unit from LNG within their system architecture. Conversely, in the case of PEMFC, determining system dimensions and weight necessitates a separate calculation owing to the absence of an inherent H
2 production unit within the cell design.
Table 5 shows the properties of a commercial battery cell [
52] used to form the stack.
The properties listed in
Table 5 pertain to a single battery cell. Based on the required battery capacity and assuming a 440 V line voltage for the ship’s grid, battery packs have been assembled from these individual cells. The constant current constant voltage (CC-CV) charging protocol has been used as the charging method, and the modelling of the battery pack has been ensured by considering this protocol. The battery voltage drop was simulated using the SoC versus Voltage curves from the manufacturer’s datasheet [
52].
The SoH curves have also been obtained from the manufacturer data sheet, and the curve slope varies depending on the C-rate (charge/discharge rate). The algorithm logic for using SoH equations is shown in the modelling section. On the other hand, the WHRS uses an organic Rankine Cycle (ORC) to produce electricity from exhaust waste heat.
Table 6 shows the exhaust mass flow rates (
) and the inlet temperature of the exhaust to the WHRS after the exhaust boiler (
) taken from the manufacturer’s datasheet.
The M/E power, speed, and load were collected from the case study vessel, and the exhaust gas amount and temperatures were interpolated from the data. The ORC model was taken from the models developed by Konur, et al. [
53]. The total volume and required area for the FC battery configurations were calculated by considering the distance of 1.8 m between each piece of equipment [
54].
2.2. Simulation Logic
An energy management strategy (EMS) algorithm and simulation designed by the authors has provided the determination processes of load-sharing, the number of generators or FCs, and battery charging/discharging conditions. The simulation was developed in Python, and the powertrain options for the hybrid marine power distribution plant were conducted using the same code infrastructure. At the beginning of the simulation, the user can adjust the FC, battery, and WHRS implementations and their capacities.
Figure 5 illustrates the simplified algorithm scheme of the simulation and EMS.
The algorithm starts with importing data and necessary libraries while setting the initial values and empty lists for the iteration. The iteration is conducted based on the size of the grid power data; the program then verifies whether WHRS is selected as a support option by the user and calculates the power produced by the system based on the ME power.
After the WHRS determination, the function decides the number of operating FCs, battery charge/discharge power, and engine load. The capacity of FCs and battery changes are determined according to the hybrid scenario and FC type, while the WHRS power availability affects the parameters’ determination. The sizes of FCs and batteries have been selected to ensure that MDEs operate outside the low-load zones. Considering the battery charging/discharging state and power, the EMS manages the battery performance. The SoC has been kept between 20% and 80% to extend the battery life.
The collected operational data includes instantaneous load increases, such as those caused by thruster usage. The algorithm determines the ship’s operation mode based on changes in the power of the M/E and A/E. The EMS evaluates the slope of power increases in the A/Es. Under near-constant operation, the FCs and WHRS, if available, are prioritised in the hierarchy. The availability of WHRS, if present in the configuration, is determined based on the operation mode and a M/E load exceeding 50%. If the slope of demand increases rapidly or the power demand surpasses the capabilities of the FCs and WHRS, the batteries are incorporated into the operation. Finally, if these measures are insufficient, the MDE is activated.
In scenarios utilising FCs, the FC charges the batteries, with the SoC-voltage curves provided earlier are used to calculate voltage drop and determine the battery’s available power. The SoH is calculated simultaneously. In the subsequent step, the required engine power is assessed to determine the number of operational D/Gs, and the HFO consumption has been estimated using the curve shown in
Figure 4.
The computed parameters within the loop are appended to pre-initialized empty lists at the start of the algorithm. At the end of each iteration, these lists are exported to MS Excel for further analysis and cleared for the next iteration. Once the total fuel consumption for the hybrid scenarios is calculated, additional evaluations are performed, including fuel tank capacity design, upstream emissions computation, EEXI/CII rating evaluation, and economic performance assessment.
2.3. Mathematical Background
This section contains the mathematical equations used in the FC, battery, WHRS, and ICE calculations. The coefficients and methods used in the environmental and economic analysis have also been indicated. In addition, the EEXI and CII computation process and the stages of the MCDM approach have been described.
2.3.1. Fuel Cell Calculations
This section demonstrates and explains the equations used in the mathematical model. Equation (1) has been employed to calculate the H
2 consumption of SOFC and PAFC.
The operation time is denoted as t in h, and the power of one FC is represented by
in kW, Lower heating value (
for the H
2 has been taken at 120,000 kJ/kg [
55], and the efficiency of fuel (
cells have been computed by applying a 0.5% degradation per 1000 h [
56]. The calculation of the tank capacities concerning the H
2-utilized scenarios has been ensured by assuming that it has been stored at the compressed state, having a density of 75 kg/m
3 [
57,
58].
The efficiency and fuel consumption values have been interpolated using the curves provided by the manufacturer [
50] for the PEMFC. Emissions of FCs (
have been calculated by using Equation (2) and the LNG consumption of PAFC has been computed by employing Equation (3) [
34].
where
represents the emission coefficient given in
Table 4, and the number of operating FCs is
. LNG consumption has been calculated by using the t of PAFC, the coefficient of LNG consumption (
) depicted in
Table 4, and 0.007 is the conversion coefficient from Nm
3 to metric tons [
59].
2.3.2. Waste Heat Recovery Model
Equation (4) computes the generated power by the WHRS (
) by using the data illustrated in
Table 6.
where
is in kg/s and
is in °C, as shown in
Table 6.
is the outlet temperature from ORC, which is taken at 100 °C, and
is the amount of thermal energy that, when pressure stays stable, a mass of exhaust emits or absorbs with an alteration in temperature and is taken at 1.089 kJ/kg.K [
60]. The efficiency of ORC (
) is taken at 13.2% from the thermodynamic model of Konur, et al. [
53].
2.3.3. Battery Model
The voltage of the battery stack has been computed by fitting the curves provided by the battery manufacturer [
52]. The EMS decides the operational state of the batteries by using the SoC, which is the rate of available battery capacity, while calculating the voltage from curves. The time-dependent SoC has been calculated with the traditional Coulomb counting method depicted in Equation (5) [
61,
62].
SoC (0) refers to the initial SoC at the beginning of the iteration, while SoC(t) represents the updated SoC at time t. The EMS maintains the battery’s SoC between 20% and 80% to minimise internal resistance, thereby preserving battery health and longevity [
61]. The coulombic efficiency has been assumed at 1 (
, the charging or discharging current is denoted as I(t), and the available battery capacity in Ah is represented by
in the formula. CC-CV charging protocol and CC discharge have been implemented to control the charging and discharging of the batteries.
The capacity reduction because of the battery degradation has been implemented in the battery model by employing the SoH curves from the battery cell manufacturer [
52]. The capacity decrease of the battery is calculated iteratively during operation, with adjustments made based on the C-rate. The SoH has been found by employing Equation (6), which is the ratio between actual battery capacity (
) after degradation and capacity at the beginning (
) of the operation [
63].
Due to lacking memory impact and having higher specific energy, lithium-ion batteries have been utilised in hybrid operation scenarios [
62]. The conversion of DC battery current to AC for grid use is assumed to utilise the SMA Sunny_SCS2900 model inverter, with an efficiency of 0.984 (at 800 V DC to 450 V AC).
2.3.4. Internal Combustion Engine Calculations
The algorithm determines the required engine power
and the number of working generators (
) in each time interval (t = 1 min). The load and power of each generator were calculated in the simulation, and their SFC was obtained by interpolating the curves shown in
Figure 4 . The load sharing has been determined by using the model presented in the study of Yuksel and Koseoglu [
45]. The load-sharing mechanism operates based on an algorithm that monitors the frequency and power of the generator; if the required power exceeds 85% of the generator’s load capacity, an additional generator is automatically started to share the load, balancing it according to their respective frequencies and power factors. The fuel consumption of ICEs (
) in t in each iteration has been calculated by using Equation (7) [
39].
2.3.5. Environmental Analysis
The operational emissions from the engines (
) has been determined by utilising the operational emission coefficients (OEC) for HFO presented in
Table 7. The upstream emissions of fuels used in ICEs and FCs have been computed using the upstream emission coefficient (UEC) in
Table 7.
Operational (tank-to-wake) emissions for ICEs have been calculated by multiplying the HFO consumption with the OEC provided in
Table 7. For FCs, manufacturer-provided coefficients and total energy production derived from the mathematical model have been used. The process is described in
Section 2.3.1. Upstream (well-to-tank) emissions have been computed by applying the UEC to operational emissions or total energy production, depending on the units specified in
Table 7.
The equivalent CO
2 (
) indicating 100 years of global warming potential (GWP100) has been calculated for consideration of both operational and upstream GHGs by using Equation (8) [
7].
The units in
are tons. The coefficients for GWP100 provided in the IMO’s LCA guidelines [
7] have been used to calculate the warming potential of N
2O and CH
4 in terms of
, as their warming potentials are approximately 260 to 273 times and 27 to 30 times higher than CO
2, respectively.
The operational and upstream emissions have been calculated for each configuration’s fuel consumption and operational duration to evaluate the overall life cycle environmental impact. By employing a streamlined approach, this methodology simplifies the assessment process, enhancing the comprehensibility of these parameters for maritime stakeholders.
Additionally, the operational CO2 emissions have been used to compute recent energy efficiency metrics, highlighting the role of presented hybrid electrification systems in achieving regulatory compliance, which is expected to become more stringent in the coming years.
2.3.6. Energy Efficiency Metrics
Equation (9) is the concept formula to compute the attained EEXI, which is the ratio of operational carbon emission to the multiplication of capacity and reference speed (
) [
67].
The capacity is DWT for the bulk carriers [
68] and
is 14.3 knots for the case study ship. CO
2 emissions were calculated by multiplying the operational CO
2 coefficient provided in
Table 7 with the HFO consumption determined through mathematical simulation. The operational data also include details on the duration of operation, expressed in hours. The attained EEXI of the base case has been compared with various hybrid scenarios to identify the configuration that achieves the most significant reduction. The required EEXI has been calculated by employing Equation (10), which is the product of the reduction factor (X) and reference EEDI line for the reference bulk carrier [
67].
X is 20% for the bulk carriers, and the coefficients in Equation (10) are also specific to the bulk carriers [
68]. The required EEXI has been calculated as an upper limit and benchmark to compare with the attained EEXI, assessing whether the vessel, under various configurations, complies with the latest technical requirements established by the IMO.
The CII is an operational measure established by the IMO, whereas the EEXI is a technical measure. Attained CII has been calculated by using Equation (11) [
69].
where the travelled distance is denoted by
and the capacity is the operational DWT depending on the loading condition of the vessel [
67]. CO
2 emissions have been calculated annually based on the yearly HFO consumption and the operational CO
2 coefficient provided in
Table 7. The attained CII of the base scenario has been compared with zero-carbon hybrid configurations to identify the hybrid system with the most significant potential reduction. The required CII has been calculated using the reference CII line for bulk carriers and Equation (12).
The CII reference line is for 2019. The required CII is calculated by applying the reduction factor (Z), starting at 5% for 2023 and increasing by 2% annually until 2026 [
69]. The required CII has been calculated to establish threshold values for ratings and to facilitate the comparison of zero-carbon configurations with the base scenario.
The CII ratings of the configurations have been determined by using the dd vectors for the reference bulk carrier taken from IMO [
70]. The ratings have been calculated by multiplying the dd vectors with the required CII after the Z has been applied according to each year [
70].
Energy efficiency metrics have been calculated to demonstrate the impact of regulatory compliance provided by hybrid electrification systems. While the environmental analysis emphasises operational CO2 emissions, the results from this analysis were utilised to calculate the EEXI and CII metrics. These metrics offer a structured approach for the maritime industry to evaluate energy efficiency, ensuring alignment with the framework established by the IMO.
2.3.7. Economic Analysis
The economic performance of the scenarios has been measured by the levelized cost of energy (LCOE) and electricity production cost (EPC). LCOE is the principal tool of choice for assessing the unit costs at the plant level of different baseload technologies throughout their operational lives [
71]. Equation (13) demonstrates the calculation of the LCOE [
72].
where the installation costs are depicted as
, fuel costs are denoted as
, and
represents the operation and maintenance spending. Generated total power
) and total t of the plant have been computed using the collected data. Discount rate (r) has been assumed at 10%, and plant lifetime (LT) has been taken at 20 years [
71,
73]. The calculation of the LCOE has been performed by accounting for annual expenses, including
and
, over the plant’s LT with a fixed r value The total of these recurring expenses, combined as
, has been divided by the cumulative energy production over the system LT to determine the LCOE.
Table 8 shows the LT,
, and
of the equipment.
has been calculated by multiplying the ratios provided in
Table 8 with the
. The analysis has been conducted using United States Dollars (USD). The exchange rate between Euro (EUR) to USD has been taken at 1.07. The prices taken from previous years have been corrected by employing the rate of the related data year and recent Chemical Engineering Plant Cost Index (CEPCI). The latest CEPCI has been announced as 800.3 for February 2024. The CEPCI values for previous years, as well as the most recent data, have been taken from Maxwell [
81].
Future projection rates for cost changes have been obtained from the literature for each specific type of equipment. For FCs, the price reduction trends of PEMFCs over time have also been assumed to apply to other types. In cases where future cost projections for specific equipment are unavailable in the literature, the costs have been considered to remain constant throughout the analysis period.
The expected LT values for FCs have been established as 40,000 h for PEMFC and PAFC and 60,000 h for SOFC. If these FCs are not projected to reach their expected lifetimes, it is assumed that they will need to be replaced within 10 years. The LT of batteries is contingent upon their hybrid configuration and is calculated based on SoH curves. In scenarios where battery usage is minimal and the calculated lifetime exceeds 10 years, it is assumed that batteries will be replaced every ten years in the analysis.
Equation (14) calculates the EPC, which is the fuel cost per kWh produced [
73]. EPC is chosen as a metric because it practically evaluates the price spent on fuel per kWh, offering a simpler and more practical alternative to the more complex LCOE.
Table 9 demonstrates the current
, the projection ratios of future fuel prices, and carbon tax costs.
The EPC calculation focuses on
and carbon taxes, with cost projection scenarios outlined in
Table 9.
for 2024 has been obtained from ShipandBunker [
82] on 18 June 2024. The values of
in
Table 9 indicate the projected annual rates of change, which the economic model uses to evaluate the scenarios for 2030 and 2050. Projection cases are classified as low, medium, and high, reflecting different trends in fuel price dynamics. The low case assumes slow increases or steep decreases in fuel prices, the medium case represents a moderate rate of price growth, and the high case anticipates rapid price increases or slower decreases. For example, in the LNG low scenario, a 2.04% annual reduction has been applied, and the values for 2030 and 2050 have been calculated.
This framework is similarly applied to carbon prices, aligning them with the corresponding fuel price scenarios based on data from the literature. Various carbon tax scenarios and projections exist in the literature, reflecting uncertainty in the direction of future prices. The analysis classifies carbon prices according to the scenarios and expectations established in the literature to encompass the diverse carbon pricing pathways.
The described economic modelling approach has been applied to account for the variability in fuel price dynamics and uncertainty of carbon taxes, enabling a comprehensive evaluation of future economic scenarios under different conditions and policy environments.
2.3.8. Technique for Order of Preference by Similarity to Ideal Solution
Using TOPSIS, a popular MCDM technique in academic research, the hybrid and conventional setups have been ranked based on various criteria. The methodology generates optimal solutions and highly understandable results by employing a straightforward approach [
87].
The selected criteria have been determined based on three primary aspects: environmental performance, economic feasibility, and space requirements. Two specific parameters represent each criterion. For environmental performance, these are total hourly CO2-eq: emissions and the sum of other hourly emissions. Economic feasibility is assessed through the LCOE and EPC metrics, depending on the financial projection scenario and year. Space requirements are evaluated using parameters such as required tank capacities, mass, and equipment volume.
All six criteria are non-beneficial, and their relative weights have been assigned using the equal weighting method (16.66% for six criteria), an objective weighting approach commonly employed in general evaluation scenarios such as this application.
The TOPSIS application in this study is specifically employed to compare many hybrid configurations, facilitating ease of understanding and interpretation. This methodology is beneficial for demonstrating variations across different economic scenarios and with increasing carbon prices. It is important to note that the weights and resulting rankings may vary depending on the decision-maker’s preferences. The TOPSIS method’s applicability and the ranking system’s clarity offer significant advantages, especially in fostering collaboration with industry partners in the maritime sector.
In the method, the best rankings are determined by finding the closest range to the positive ideal solution (
) or the furthest extent to the negative ideal solution (
). The benefits are maximised by
while the costs are scaled up by the
. The methodology starts with the creation of the decision matrix and applying the normalisation process shown in Equation (15) to the matrix [
88].
The normalised matrix element is denoted by
, and
is the member of the decision matrix. The normalised decision matrix is multiplied by the criteria weights in the next step. The determination of
and
, depending on whether the criterion is beneficial or non-beneficial, is the following stage. For the non-beneficial or cost-type criterion,
is the minimum and
is the maximum value in the decision matrix, while the beneficial parameter is the opposite. The Euclidean distance between each weighted normalised matrix member (
) and
is
, and similarly
is between each member and
.
and
are calculated by applying Equations (16) and (17) [
87,
88].
The rank of each configuration is determined by sorting the relative closeness coefficient (
) computed by Equation (18) [
87,
89].
2.3.9. Uncertainty Analysis
Uncertainty quantifies the reliability of a result and is essential for evaluating the data’s suitability for informed decision-making in areas such as health, safety, commerce, and scientific research [
90]. Among statistical methods, uncertainty analysis effectively identifies scenarios influenced by uncertainties and enhances data accuracy [
91]. Different uncertainty levels are combined using Equation (19) [
92].
In Equation (19), U values denote the fractional uncertainties of individual independent variables (x
1, x
2,…x
n), U
R presents the uncertainty of the combined computation, while R corresponds to the result or utilised value for each independent parameter [
93].
An uncertainty analysis of the mathematical model used to calculate fuel consumption, as described in
Section 2.2, has been performed to evaluate the reliability of the computations. Two primary sources of uncertainty are identified in the simulation. First, the ICE fuel consumption is derived from SFC curves provided by the manufacturer for hybrid configurations. When the model is applied to these curves for the base case, the error rate between experimental data and modelling results is 5.63%. Second, as specified in the data sheets, the FC efficiencies have an associated error rate of 2%. Using Equation (19), the mathematical model demonstrates a combined uncertainty of 5.98%.