esa-sceva/satcom-chunk-collection huggingface dataset:
# Advances in Graphene Field Effect Transistors (FETs) for Annine Neurotransmitter Sensing
## 2 Problem Outline
### Graphene Channel Functionalisation  
Graphene has a strong Van der Waal force between its carbon network (C-C) that produces severe aggregation in the composite matrix; this results in graphene layers restacking to create graphite [120; 121]. Although graphene has a large surface area, the aromatic character of the C-C bonds and delocalised \(\pi\)-bonding system contribute to the chemical stability and render chemical inertness. This prevents graphene from establishing covalent links with other materials and limits its direct chemical reactivity [122]. Graphene materials typically have functional groups located at holes, edges, curvatures in the basal plane, and chemical contaminants, which are reactive to biomolecules [122]. These functional groups typically include hydroxyl (-OH), carboxyl (-COOH), and epoxy groups (-COC-) [123], and they enable binding to a wide range of compounds, particularly biomolecules for a variety of biomedical applications [124]. Thus, to facilitate the biomolecule attachment and detection of target analytes, the graphene channel is functionalised, and the bioreceptors are immobilised onto it. Through chemical modification or molecule adsorption, graphene can be functionalised to induce bandgap engineering effects and doping, thereby modifying graphene's electrical characteristics [125]. Through adsorption, the target biomarker is induced by immobilising a highly specific bioreactor to the graphene surface to achieve chemical specificity. Amino acids, enzymes, antibodies, aptamers, and other selective and specialised molecules can all function as such receptors [126]. Conversely, if a linker molecule is needed, the graphene channel is functionalised through non-covalent binding to the graphene via weak Van der Waals interactions or through covalent binding to the carbon atoms at defects in the hexagonal matrix [125].
## 4 Analysis of Factors Influencing Anchoring Performance  
### Strength of Grouting Material  
The load values of steel bars and corresponding elongations were recorded during the testing process with digital pressure and displacement gauges. Subsequently, load-displacement curves were generated. The analysis evaluated the effects of the grouting material strength, bonding length of grout anchor steel bars, and the spacing of U-shaped stirrups on the anchorage performance of the test specimens. Figure 9 illustrates the load-displacement curves for specimens utilizing grouting materials of varying strengths. The following observations were made:  
(1) The load-displacement curve can generally be segmented into four distinct phases. During the initial loading phase, the specimen remains in an elastic stage, exhibiting an almost linear relationship between load and displacement. As the load increases, the  
Figure 9: Load-displacement curves of specimens with different strengths of grouting material. (a) Specim A-0.4; (b) Specim A-0.6; (c) Specim A-0.8; (d) Specim A-1.0; (e) Specim A-1.2.  
slope of the curve diminishes, signaling the specimen's transition into the yield stage, characterized by a yield plateau. This yield stage is modulated by the strength of the grouting material and is represented as a slanted straight line, indicative of stable load-bearing performance. Following the plastic deformation in the yield stage, the grout anchor steel bars enter a strengthening stage, where displacement consistently rises as the load intensifies. Upon attaining the ultimate state, the steel bars commence necking, eventually leading to pull-out and the specimen's failure.  
(2) The strength of the grouting material exerts a considerable impact on the load-displacement curves. Analysis of results from specimens with anchorage lengths of 0.4 and 0.6 L\({}_{\text{ab}}\) reveals that medium-strength C-type grouting material offers enhanced anchorage performance relative to low-strength A- and B-type materials. Although ultimate displacements across the specimens are essentially uniform, the requisite applied load shows a notable increase. Further comparative analysis of specimens with anchorage lengths of 0.8, 1.0, and 1.2 L\({}_{\text{ab}}\) confirms the persisting influence of grouting material strength. However, as the anchorage length extends, the disparity in the required applied load for equivalent displacement diminishes.  
(3) When all other variables remain constant, a higher grouting material strength results in a greater bonding force exerted on the steel bars, thus yielding superior anchorage performance. In addition, a decrease in ultimate displacement is observed when the specimen undergoes failure.
# Plants as Symbols of Power in the Achaemenid Iconography of Ancient Persian Monuments
## 4 Discussion
### The Date Palm as a Reinterpreted Metamorphic Tree of Life in Middle Eastern Cultures  
The importance of the date palm in this geographical context can be explained by its value as an economic plant and by its resultant symbolic attributes. Subfossil desiccated fruits and/or seeds have been recovered from excavations at Susa (Iran) and in other areas of the Middle East [141]. _Phoenix dactylifera_ is one of the few arboreal species that is able to survive harsh conditions, as long as there is abundant underground water. This palm requires a long and intense hot summer with little rain and very low humidity during the period following pollination [142], and its ability to thrive in the arid Mesopotamian environment made it a powerful symbol of life in the midst of a challenging landscape [97].  
The plant has been the subject of a complex chain of interlocking associations, including Istar, fertility, and kingship [22], and it was also identified as the 'Sacred Tree' or 'Tree of Life' of the older Assyrian civilization, perceived as having apotropaic powers [30; 95; 143]. It has been suggested that, during the Assyrian period, the date palm and its ritual fertilization were so important to society that it must have led to the plant receiving the symbolic status of a sacred tree [141]. In Egypt, the date palm was a symbol of fertility and divinity, with [PERSON] and [PERSON] portrayed together with palm leaves [18; 136]. Later, these concepts were transferred into Greek, Roman, and Christian cultures, where the date palm continues to hold great symbolic importance. In different cultures around the Mediterranean and in West Asia, palms are defined culturally as 'keystone species', i.e., species whose existence and symbolic value are essential to the stability of a cultural group over time [144; 145].  
The metamorphic shape of date palms represents another example of media-specific programs in Achaemenid art [22]. Iranian kings had a special date palm known as the 'Royal' palm. It was special because, as soon as a tree died, another one grew out of its roots. Because of this, the date palm was associated with fertility, prosperity, and purity, and therefore, it was held to be an emblem of immortality and royalty among ancient Iranians and often used in Zoroastrian religious ceremonies, representing resistance to evil forces [146]. Pomegranates and date palms were sometimes planted together in Persian gardens as symbols of paradise [42], and Fire Temples often have date palms growing on their premises [147].
# Passive Earth Pressure and Soil Arch Shape: A Two-Dimensional Analysis
## 2 Derivation of Equilibrium Differential Equations and Solution for Passive Earth Pressure  
### Establishment of Equilibrium Differential Equations  
The problem of passive earth pressure acting on a retaining wall is analyzed under the following assumptions: (1) The problem is idealized as a two-dimensional plane strain condition. (2) The backfill material is a homogeneous, isotropic sand (cohesionless). (3) The shear strength behavior of the backfill adheres to the Mohr-Coulomb failure criterion. (4) The retaining wall is vertical, with a rough back surface (mobilizing friction), and the backfill surface is horizontal. (5) The potential sliding surface within the backfill is assumed to be a plane originating from the wall heel.  
Figure 1b illustrates the potential sliding plane and stress conditions of an arbitrary differential element (dxdz) within the soil mass when the passive state is achieved. A Cartesian coordinate system (\(x\), \(z\)) is established with its origin at the wall heel, where \(z\) is positive upwards. Considering the differential element located at coordinates (\(x\), \(z\)) within the sliding soil mass, its stress state is shown in Figure 1b. Based on continuum mechanics principles, the equilibrium equations are established as follows:  
\[\frac{\partial\sigma_{x}}{\partial x}-\frac{\partial\tau_{zx}}{\partial z}=0, \tag{1}\]  
Figure 1: Schematic comparison of analysis methods: (**a**) traditional horizontal layer analysis; (**b**) proposed 2D differential element approach.  
\[\frac{\partial\sigma_{z}}{\partial z}-\frac{\partial\tau_{xz}}{\partial x}=-\gamma, \tag{2}\]  
where \(\sigma_{x}\) is the horizontal normal stress, \(\sigma_{z}\) is the vertical normal stress, \(\tau_{zx}\) and \(\tau_{xz}\) are the shear stress, and \(\gamma\) is the unit weight of the soil. Compressive normal stress is adopted as positive in this paper.
# The Non-Linear Impact of Industry 4.0 on Carbon Emissions in China's Logistics Sector
## 4 Discussion  
### Interpretation of Results  
The results indicated the positive and negative effects of Industry 4.0 on the carbon emissions of logistics. The polluting aspect of production systems was averted by the application of more advanced technologies. This generated a U-shaped curve between Industry 4.0 and carbon emissions, which suggests that though the initial stages of technology implementation might increase pollution, sustainability could eventually get better. This starting point can be understood as the heavy energy requirements and operational inefficiencies that go along with the launch of new technologies [24]. Nevertheless, by successfully addressing these obstacles and developing technologies, the result is that there are remarkable efficiency gains and massive carbon emission reductions to be gained. Therefore, the implication here is that a systematic, stage-by-stage mechanism of the Industry 4.0 technologies is an assured and successful strategy for ensuring that the short-term upsurge in CO2 emissions is countered by the long-term gains from sustainability.  
The boost in production efficiency, enlargement of the business operations volume, and upgrade of information system harmony are the prime factors that enable Industry 4.0 to contribute in the sector of carbon emissions. All these factors have their inputs in terms of finally cutting down emissions by maximizing the cost-effectiveness of the use of resources, minimizing waste, and cutting down on harmful emissions through improved decision-making at all levels from manufacturers to end-users [25]. This shows that the success of Industry 4.0 as an environmental solution will depend on the ability of logistics managers to accommodate these factors in the operation of Industry 4.0.  
This discussion will highlight several key implications of the findings. First, the non-linear relationship between Industry 4.0 adoption and carbon emissions suggests that policymakers should adopt a phased approach to technology integration, focusing initially on improving operational efficiency before scaling up automation and AI deployment. Second, the significant regional disparities in technological readiness and environmental outcomes indicate the need for region-specific policies that address local challenges and leverage regional strengths. Finally, this study contributes to the broader literature on sustainable logistics by providing empirical evidence of the environmental impact of Industry 4.0 in a major emerging economy.
## 2 Materials and Methods
### Soil Sampling, Total Carbon Analysis and Spectral Measurement  
A total of 70 samples were taken from the sites and three soil layers were sampled at depths of 0-5, 5-20, and 20-40 cm. The sampling strategy was selected to represent different conditions of the native forest, from undisturbed to degraded (Figure 1, for details see [27]). The samples were kept in plastic bags and stored at -4 \({}^{\circ}\)C for later analysis. Later, the samples were air-dried and put through a 2-mm sieve in order to minimize spectral variation due to fresh organic matter, soil moisture and soil aggregates. One portion of the sample was reserved for analysis and the other for spectral scanning. Total carbon (TC) was obtained by dry combustion method [29] using an elemental analyzer (model Leco CN-2000, macro-analyzer, LECO Corporation, Saint Joseph, Michigan, USA). All TC values were combined in a unique data set that contained the entire range of all depths and both soil types. Samples for scanning were oven-dried at 60 \({}^{\circ}\)C for 48 h to standardize the moisture level, then were set in petri dishes (60 \(\times\) 15 mm) and flattened with a spatula. Thirty-six Andisol samples were taken and 34 Ultisol. Each depth was represented by twelve samples, except for the depths of 5-20 and 20-40 cm for Ultisol, where 11 samples were selected for each one.  
Spectral reflectance was measured in the VIS-NIR range (350-1075 nm) at 1-nm intervals using a spectroadiometer (HandHeld 2: Hand-held VNIR, ASD-FieldSpec(r), ASD, Boulder, Colorado, USA). We used this interval to detect possible sharp peaks in the spectral. The sensor was located vertically at a distance of 5 cm from the soil sample and it was fixed in a tripod, then a Spectralon panel was used as white reference before sample scans. Outdoor scanning was performed using the natural  
Figure 1: Location of the study sites. Two regions were selected; Region VIII (Biobio) and Region IX (Araucania) which are located in the Andean and coastal ranges of Chile, respectively. In the box, a representation of the different _Nothofagus obliqua_ forest conditions is shown for where the soil samples were extracted.  
source of light at 3:00 p.m. on a sunny day. A dark background was used to minimize the influence of ambient light, and to record the soil reflectance provided by natural illumination. Ten consecutive scans were averaged and recorded for each sample.
# Strength Analysis of Cylindrical Shells with Tangential Nozzles under Internal Pressure
## 4 Regression of the Strength-Weakening Coefficient
### Numerical Verification of Regression Equations of the Strength-Weakening Coefficient  
In order to validate the accuracy and applicability of the regression equation for the strength-weakening coefficient, four finite element models are redesigned within the dimensionless parameter range corresponding to the formula. Both regression equation calculations and the finite element limit-load analyses are performed and compared. The results are shown in Table 4. It can be seen that the results of the regression equations calculation and the finite element simulation agree well with each other with a relative difference of less than 4%, meaning the equations are accurate enough for engineering application.  
Applicability of the Regression Equations of the Strength-Weakening Coefficient for Different Shell Diameters  
The previous finite element analysis and limit-load calculations are based on the cylindrical shell diameter \(D_{i}=1000\) mm but, due to the use of dimensionless parameters, the results are applicable to other shell diameters.  
Table 5 shows the calculation results where \(d_{o}/D_{i}\), \(t/T\) and \(D_{i}/T\) are the same, but the shell diameters are 500 mm, 1000 mm and 2000 mm. It is seen that for the cylinder without nozzles when the diameter-thickness ratio \(D_{i}/T\) is kept constant but the diameter \(D_{i}\) is changed, the limit-load value is unchanged, which is 6.48 MPa. For the cylinder shells with tangential nozzles, when \(d_{o}/D_{i}\), \(t/T\) and \(D_{i}/T\) are the same, the limit load and the strength-weakening coefficient are basically the same when changing the shell diameter \(D_{i}\), and the relative error between the finite element solution and the formula solution for the strength-weakening coefficient is within 4%. Therefore, for the tangential nozzle structure with different shell diameters, the strength design method is also applicable when the three variables \(d_{o}/D_{i}\), \(t/T\) and \(D_{i}/T\) are within the applicable range specified in this paper.  
\begin{table}
\begin{tabular}{c c c c c c} \hline \hline \(d_{o}/D_{i}\) & \(t/T\) & \(D_{i}/T\) & \begin{tabular}{c} **Limit Load** \\ _P/MPa_ \\ \end{tabular} & \begin{tabular}{c} **The Finite Element Solution of** \\ _Strength–Weakening_ \\ **Coefficient \(K\)/\%** \\ \end{tabular} & \
\begin{tabular}{c} **The Formula Solution of** \\ **Strength–Weakening** \\ **Coefficient \(K\)/\%** \\ \end{tabular} &
\begin{tabular}{c} **Relative** \\ **Difference/\%** \\ \end{tabular} \\ \hline
0.13 & 0.8 & 90.91 & 5.90 & 17.18 & 17.10 & 0.50 \\
0.27 & 0.8 & 111.11 & 3.21 & 45.01 & 44.44 & 1.28 \\
0.18 & 1.4 & 90.91 & 6.09 & 14.49 & 14.41 & 0.56 \\
0.22 & 1.4 & 111.11 & 4.52 & 22.54 & 22.30 & 1.05 \\ \hline \hline \end{tabular}
\end{table}
Table 4: Verification of regression equations.
## 3 Results
### Discussion
#### 3.4.1 Point vs. Full-Field Measurements  
As mentioned in Section 2.2, LVDTs were fixed at the center of the panel and at the four panel corners to track the deflection of the element. The central LVDT stands a few millimeters further from the point defined at the DIC map as _Pmiddle_ (see Figure 5a). The LVDT and DIC measurements were proven to be identical if the rigid body motion of the panel is excluded. However, in this section, the limited information derived from the point measurements, such as of the LVDT or of the _DIC Pmiddle_ point, should be discussed. In Figure 5d, the out-of-plane displacement (rigid body motion excluded) at each loading step for the _Pmiddle_ points at both the REF (blue) and IID (red) is projected. It is shown that the out-of-plane displacement is almost identical for the REF and the IID case, therefore by measuring only at a random point in the middle of the panel one cannot detect the local debonding that occurs aside. In other words, point measurements are not capable of detecting a stochastic premature debonding failure, since the debonding onset location cannot be predicted. Therefore, the essential need for full-field inspection methods, such as AE and DIC, is evident. Only by monitoring the whole area under investigation can one pinpoint local debonding that only locally and stochastically occurs.
## 1 Introduction
Therefore, the main contributions of this paper are:  
* In-depth analysis of the antenna from the connectivity perspective with respect to possible beam steering in horizontal and elevation directions;
* Presentation of an approach for DoA estimation relying solely on RSS values gathered at the antenna output, which is a prerequisite for energy-efficient WSN nodes having DoA functionality [9; 10], that is suitable for the antenna and can provide acceptable DoA estimation results also for low \(\theta\) angles and are free from ambiguities for lower SNR values;
* Proposal of a detailed DoA algorithm performance testing method for more accurate DoA estimation accuracy assessment that involves all \(\theta\) angles to address strong error variation at low \(\theta\) angles. The rest of this paper is organized as follows: in Section 2 the two-row ESPAR antenna is described together with its simulated and measured radiation patterns as well as their influence on the overall connectivity in WSN-based IoT setups, in which the positions of nodes are not restricted to the horizontal plane only. Section 3 describes a PPCC-MCP algorithm and its proposed generalization for the usage with the two-row ESPAR antenna. Results obtained using a new RSS-based DoA estimation accuracy assessment involving thorough testing conducted along the elevation direction are presented in Section 4, while Section 5 presents concluding remarks.
## 3 Materials and Methods
### Control System Design
#### 3.3.4 PID Coefficient Determination  
In designing the PID controller for shuttle shifting and clutch actuator control, the determination of PID coefficients is most important [43]. The initial PID coefficients were determined using the Ziegler-Nichols (Z-N) method and Equations (16)-(18) based on the delay time (\(L\)) and time constant (\(\tau\)). To determine the PID coefficients, the response and stability of the system performance were analyzed, in the order of the \(\mathrm{K_{P}}\), \(\mathrm{K_{I}}\), and \(\mathrm{K_{D}}\) coefficients [30]. \(\mathrm{K_{P}}\) was determined by selecting an initial \(\mathrm{K_{I}}\) and \(\mathrm{K_{D}}\), and \(\mathrm{K_{I}}\) was determined using the determined \(\mathrm{K_{P}}\) and initial \(\mathrm{K_{D}}\). Finally, the \(\mathrm{K_{D}}\) coefficients were determined using the determined \(\mathrm{K_{P}}\) and \(\mathrm{K_{I}}\). Figure 8a shows the procedure of determining the PID coefficients. Lower overshoot, settling time, and steady-state error lead to better control performance parameters of the actuators. In this study, the shuttle shifting actuator was controlled by overdamping with a minimal settling time and steady-state error, regardless of overshoot. The clutch actuator was controlled by underdamping with no overshoot, as well as minimal settling time and steady-state error, as oscillation should not occur, as shown in Figure 8b. A stability evaluation was also conducted by calculating relative stability using the Nyquist stability criterion, which is one of the basic tools for stability criteria in the frequency domain using the two parameters of gain margin and phase margin. This criterion is useful for determining the stability of a feedback control system [44].  
\[K_{P}=1.2\frac{\tau}{L}, \tag{16}\]  
\[K_{I}=\frac{K_{P}}{2L}, \tag{17}\]  
\[K_{d}=0.5K_{P}L, \tag{18}\]  
where \(L\) is the delay time (s).  
Figure 7: Block diagram of transfer function of the electric actuator system.
###### Abstract  
The aim of this study was to analyze the effects of the playing position (backs vs. pivots vs. wings) and the player role (starter vs. non-starter) on the internal match load and well-being status of female handball players after official matches. Fourteen female handball players from the Spanish 2 nd Division were monitored during a half-season (13 matches, \(n=102\) individual observations) using the rate of perceived exertion (match RPE) and the Hooper questionnaire in MD+1 and MD+2. Differences in match RPE according to playing positions and player roles were determined by one-way ANOVA or by a paired \(t\)-test, respectively. Differences in well-being status according to playing positions or player roles and time (MD+1 and MD+2) were assessed through mixed two-way ANOVA. Furthermore, partial eta-squared (\(\eta p^{2}\)) and Cohen's d (ES) were calculated and interpreted using [PERSON] categorization criteria. Backs registered moderately more match RPE compared to pivots (\(p<0.05\), ES = 0.84). By contrast, wings experienced the highest values of fatigue and muscle soreness in MD+1 and MD+2 compared to all other playing positions (\(p<0.05\), ES = 0.66-0.93). Also, the wings reported moderately higher Hooper index scores in MD+1 and MD+2 than backs (\(p<0.01\), ES = 0.73-0.77). In relation to the player role, starters reported higher absolute values of match RPE, fatigue, muscle soreness, and the Hooper index in MD+1 compared to non-starters (\(p<0.05\), ES = 0.25-0.29). Additionally, regardless of the playing position and the role, all of the players reported moderately less fatigue and Hooper index scores in MD+2 compared to MD+1 (\(p<0.05\), ES = 0.66-1.34). Therefore, coaches and practitioners should consider the internal match load and well-being status of players to implement different training stimuli (e.g., recovery or compensatory strategies) in MD+1 according to playing positions and player roles.  
Keywords:load monitoring; workload; fatigue; sleep; muscle soreness; team sport; women licenses/by/4.0/. +
Footnote †: journal: Applied sciences